Applied petroleum reservoir engineering third edition This page intentionally left blank Applied petroleum reservoir engineering third edition Ronald E. Terry J. Brandon Rogers New York•Boston•Indianapolis•SanFrancisco Toronto•Montreal•London•Munich•Paris•Madrid Capetown•Sydney•Tokyo•Singapore•MexicoCity Manyofthedesignationsusedbymanufacturersandsellerstodistinguish theirproductsareclaimedastrademarks.Wherethosedesignationsappearinthisbook,andthepublisherwasawareofatrademarkclaim,the designationshavebeenprintedwithinitialcapitallettersorinallcapitals. Executive Editor Bernard Goodwin Theauthorsandpublisherhavetakencareinthepreparationofthisbook, butmakenoexpressedorimpliedwarrantyofanykindandassumenoresponsibilityforerrorsoromissions.Noliabilityisassumedforincidental orconsequentialdamagesinconnectionwithorarisingoutoftheuseof theinformationorprogramscontainedherein. Project Editor Elizabeth Ryan Forinformationaboutbuyingthistitleinbulkquantities,orforspecial salesopportunities(whichmayincludeelectronicversions;customcover designs;andcontentparticulartoyourbusiness,traininggoals,marketing focus, or branding interests), please contact our corporate sales departmentatcorpsales@pearsoned.comor(800)382-3419. For government sales inquiries, please contact governmentsales@pearson ed.com. ForquestionsaboutsalesoutsidetheU.S.,pleasecontactinternational@ pearsoned.com. VisitusontheWeb:informit.com/ph Library of Congress Cataloging-in-Publication Data Terry, Ronald E. Appliedpetroleumreservoirengineering/RonaldE.Terry,J.Brandon Rogers.—Thirdedition. pages cm Original edition published:Applied petroleum reservoir engineering / byB.C.CraftandM.F.Hawkins.1959. Includesbibliographicalreferencesandindex. ISBN978-0-13-315558-7(hardcover:alk.paper) 1. Petroleum engineering. 2. Oil reservoir engineering. I. Rogers, J.Brandon.II.Craft,B.C.(BenjaminCole)III.Title. 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To Rebecca and JaLeen This page intentionally left blank Contents Preface PrefacetotheSecondEdition AbouttheAuthors Nomenclature xiii xv xvii xix Chapter 1 Introduction to Petroleum Reservoirs and Reservoir Engineering 1.1 IntroductiontoPetroleumReservoirs 1.2 HistoryofReservoirEngineering 1.3 IntroductiontoTerminology 1.4 ReservoirTypesDefinedwithReferencetoPhaseDiagrams 1.5 ProductionfromPetroleumReservoirs 1.6 PeakOil Problems References 1 1 4 7 9 13 14 18 19 Chapter 2 Review of Rock and Fluid Properties 2.1 Introduction 2.2 ReviewofRockProperties 2.2.1 Porosity 2.2.2 IsothermalCompressibility 2.2.3 FluidSaturations 2.3 ReviewofGasProperties 2.3.1 IdealGasLaw 2.3.2 SpecificGravity 2.3.3 RealGasLaw 2.3.4 FormationVolumeFactorandDensity 2.3.5 IsothermalCompressibility 2.3.6 Viscosity 21 21 21 22 22 24 24 24 25 26 34 35 41 vii viii Contents 2.4 ReviewofCrudeOilProperties 2.4.1 SolutionGas-OilRatio,Rso 2.4.2 FormationVolumeFactor,Bo 2.4.3 IsothermalCompressibility 2.4.4 Viscosity 2.5 ReviewofReservoirWaterProperties 2.5.1 FormationVolumeFactor 2.5.2 SolutionGas-WaterRatio 2.5.3 IsothermalCompressibility 2.5.4 Viscosity 2.6 Summary Problems References Chapter 3 The General Material Balance Equation 3.1 Introduction 3.2 DerivationoftheMaterialBalanceEquation 3.3 UsesandLimitationsoftheMaterialBalanceMethod 3.4 TheHavlenaandOdehMethodofApplying theMaterialBalanceEquation References Chapter 4 Single-Phase Gas Reservoirs 4.1 Introduction 4.2 CalculatingHydrocarboninPlaceUsingGeological, Geophysical,andFluidPropertyData 4.2.1 CalculatingUnitRecoveryfromVolumetricGasReservoirs 4.2.2 CalculatingUnitRecoveryfrom GasReservoirsunderWaterDrive 4.3 CalculatingGasinPlaceUsingMaterialBalance 4.3.1 MaterialBalanceinVolumetricGasReservoirs 4.3.2 MaterialBalanceinWater-DriveGasReservoirs 4.4 TheGasEquivalentofProducedCondensateandWater 4.5 GasReservoirsasStorageReservoirs 44 44 47 51 54 61 61 61 62 63 64 64 69 73 73 73 81 83 85 87 87 88 91 93 98 98 100 105 107 Contents 4.6 AbnormallyPressuredGasReservoirs 4.7 LimitationsofEquationsandErrors Problems References ix 110 112 113 118 Chapter 5 Gas-Condensate Reservoirs 5.1 Introduction 5.2 CalculatingInitialGasandOil 5.3 ThePerformanceofVolumetricReservoirs 5.4 UseofMaterialBalance 5.5 ComparisonbetweenthePredictedandActual ProductionHistoriesofVolumetricReservoirs 5.6 LeanGasCyclingandWaterDrive 5.7 UseofNitrogenforPressureMaintenance Problems References 121 121 124 131 140 Chapter 6 Undersaturated Oil Reservoirs 6.1 Introduction 6.1.1 OilReservoirFluids 6.2 CalculatingOilinPlaceandOilRecoveriesUsing Geological,Geophysical,andFluidPropertyData 6.3 MaterialBalanceinUndersaturatedReservoirs 6.4 Kelly-SnyderField,CanyonReefReservoir 6.5 TheGloyd-MitchellZoneoftheRodessaField 6.6 Calculations,IncludingFormationandWaterCompressibilities Problems References 159 159 159 Chapter 7 Saturated Oil Reservoirs 7.1 Introduction 7.1.1 FactorsAffectingOverallRecovery 7.2 MaterialBalanceinSaturatedReservoirs 7.2.1 TheUseofDriveIndicesinMaterialBalanceCalculations 199 199 199 200 202 143 147 152 153 157 162 167 171 177 184 191 197 x Contents 7.3 MaterialBalanceasaStraightLine 7.4 TheEffectofFlashandDifferentialGasLiberationTechniques andSurfaceSeparatorOperatingConditionsonFluidProperties 7.5 TheCalculationofFormationVolumeFactorandSolution Gas-OilRatiofromDifferentialVaporizationandSeparatorTests 7.6 VolatileOilReservoirs 7.7 MaximumEfficientRate(MER) Problems References Chapter 8 Single-Phase Fluid Flow in Reservoirs 8.1 Introduction 8.2 Darcy’sLawandPermeability 8.3 TheClassificationofReservoirFlowSystems 8.4 Steady-StateFlow 8.4.1 LinearFlowofIncompressibleFluids,SteadyState 8.4.2 LinearFlowofSlightlyCompressibleFluids,SteadyState 8.4.3 LinearFlowofCompressibleFluids,SteadyState 8.4.4 PermeabilityAveraginginLinearSystems 8.4.5 FlowthroughCapillariesandFractures 8.4.6 RadialFlowofIncompressibleFluids,SteadyState 8.4.7 RadialFlowofSlightlyCompressibleFluids,SteadyState 8.4.8 RadialFlowofCompressibleFluids,SteadyState 8.4.9 PermeabilityAveragesforRadialFlow 8.5 DevelopmentoftheRadialDiffusivityEquation 8.6 TransientFlow 8.6.1 RadialFlowofSlightlyCompressibleFluids,TransientFlow 8.6.2 RadialFlowofCompressibleFluids,TransientFlow 8.7 Pseudosteady-StateFlow 8.7.1 RadialFlowofSlightlyCompressibleFluids, Pseudosteady-StateFlow 8.7.2 RadialFlowofCompressibleFluids,Pseudosteady-StateFlow 8.8 ProductivityIndex(PI) 8.8.1 ProductivityRatio(PR) 206 209 215 217 218 220 224 227 227 227 232 236 236 237 238 242 244 246 247 248 249 251 253 254 260 261 262 264 264 266 Contents 8.9 Superposition 8.9.1 SuperpositioninBoundedorPartiallyBoundedReservoirs 8.10 IntroductiontoPressureTransientTesting 8.10.1 IntroductiontoDrawdownTesting 8.10.2 DrawdownTestinginPseudosteady-StateRegime 8.10.3 SkinFactor 8.10.4 IntroductiontoBuildupTesting Problems References xi 267 270 272 272 273 274 277 282 292 Chapter 9 Water Influx 9.1 Introduction 9.2 Steady-StateModels 9.3 Unsteady-StateModels 9.3.1 ThevanEverdingenandHurstEdgewaterDriveModel 9.3.2 BottomwaterDrive 9.4 Pseudosteady-StateModels Problems References 295 295 297 302 303 323 346 350 356 Chapter 10 The Displacement of Oil and Gas 10.1 Introduction 10.2 RecoveryEfficiency 10.2.1 MicroscopicDisplacementEfficiency 10.2.2 RelativePermeability 10.2.3 MacroscopicDisplacementEfficiency 10.3 ImmiscibleDisplacementProcesses 10.3.1 TheBuckley-LeverettDisplacementMechanism 10.3.2 TheDisplacementofOilbyGas,withandwithout GravitationalSegregation 10.3.3 OilRecoverybyInternalGasDrive 10.4 Summary Problems References 357 357 357 357 359 365 369 369 376 382 399 399 402 xii Contents Chapter 11 Enhanced Oil Recovery 11.1 Introduction 11.2 SecondaryOilRecovery 11.2.1 Waterflooding 11.2.2 Gasflooding 11.3 TertiaryOilRecovery 11.3.1 MobilizationofResidualOil 11.3.2 MiscibleFloodingProcesses 11.3.3 ChemicalFloodingProcesses 11.3.4 ThermalProcesses 11.3.5 ScreeningCriteriaforTertiaryProcesses 11.4 Summary Problems References 405 405 406 406 411 412 412 414 421 427 431 433 434 434 Chapter 12 History Matching 12.1 Introduction 12.2 HistoryMatchingwithDecline-CurveAnalysis 12.3 HistoryMatchingwiththeZero-Dimensional SchilthuisMaterialBalanceEquation 12.3.1 DevelopmentoftheModel 12.3.2 TheHistoryMatch 12.3.3 SummaryCommentsConcerningHistory-MatchingExample Problems References 437 437 438 441 441 443 465 466 471 Glossary 473 Index 481 Preface Asinthefirstrevision,theauthorshavetriedtoretaintheflavorandformatoftheoriginaltext.The textcontainsmanyofthefieldexamplesthatmadetheoriginaltextandthesecondeditionsopopular. Thethirdeditionfeaturesanintroductiontokeytermsinreservoirengineering.Thisintroductionhasbeendesignedtoaidthosewithoutpriorexposuretopetroleumengineeringtoquickly becomefamiliarwiththeconceptsandvocabularyusedthroughoutthebookandinindustry.Inaddition,amoreextensiveglossaryandindexhasbeenincluded.Thetexthasbeenupdatedtoreflect modernindustrialpractice,withmajorrevisionsoccurringinthesectionsregardinggascondensate reservoirs,waterflooding,andenhancedoilrecovery.Thehistorymatchingexamplesthroughout thetextandculminatinginthefinalchapterhavebeenrevised,usingMicrosoftExcelwithVBAas theprimarycomputationaltool. Thepurposeofthisbookhasbeen,andcontinuestobe,toprepareengineeringstudentsand practitionerstounderstandandworkinpetroleumreservoirengineering.Thebookbeginswithan introductiontokeytermsandanintroductiontothehistoryofreservoirengineering.Thematerial balanceapproachtoreservoirengineeringiscoveredindetailandisappliedinturntoeachoffour typesofreservoirs.Thelatterhalfofthebookcoverstheprinciplesoffluidflow,waterinflux,and advanced recovery techniques.The last chapter of the book brings together the key topics in a historymatchingexercisethatrequiresmatchingtheproductionofwellsandpredictingthefuture productionfromthosewells. Inshort,thebookhasbeenupdatedtoreflectcurrentpracticesandtechnologyandismore readerfriendly,withintroductionstovocabularyandconceptsaswellasexamplesusingMicrosoft ExcelwithVBAasthecomputationaltool. —Ronald E. Terry and J. Brandon Rogers xiii This page intentionally left blank Preface to the Second Edition ShortlyafterundertakingtheprojectofrevisingthetextApplied Petroleum Reservoir Engineering byBenCraftandMurrayHawkins,severalcolleaguesexpressedthewishthattherevisionretain theflavorandformatoftheoriginaltext.IamhappytosaythatIhaveattemptedtodojustthat. Thetextcontainsmanyofthefieldexamplesthatmadetheoriginaltextsopopularandstillmore havebeenadded.Therevisionincludesareorganizationofthematerialaswellasupdatedmaterial inseveralchapters. Thechapterswerereorganizedtofollowasequenceusedinatypicalundergraduatecoursein reservoirengineering.Thefirstchapterscontainanintroductiontoreservoirengineering,areview offluidproperties,andaderivationofthegeneralmaterialbalanceequation.Thenextchapters present information on applying the material balance equation to different reservoir types.The remainingchapterscontaininformationonfluidflowinreservoirsandmethodstopredicthydrocarbonrecoveriesasafunctionoftime. Thereweresomeproblemsintheoriginaltextwithunits.Ihaveattemptedtoeliminatethese problemsbyusingaconsistentdefinitionofterms.Forexample,formationvolumefactorisexpressedinreservoirvolume/surfaceconditionvolume.Aconsistentsetofunitsisusedthroughout thetext.TheunitsusedareonesstandardizedbytheSocietyofPetroleumEngineers. Iwouldliketoexpressmysincereappreciationtoallthosewhohaveinsomepartcontributedtothetext.Fortheirencouragementandhelpfulsuggestions,Igivespecialthankstothefollowingcolleagues:JohnLeeatTexasA&M;JamesSmith,formerlyofTexasTech;DonGreenand FloydPrestonoftheUniversityofKansas;andDavidWhitmanandJackEversoftheUniversity ofWyoming. —Ronald E. Terry xv This page intentionally left blank About the Authors Ronald E. TerryworkedatPhillipsPetroleumresearchingenhancedoilrecoveryprocesses.He taughtchemicalandpetroleumengineeringattheUniversityofKansas;petroleumengineeringat theUniversityofWyoming,wherehewrotethesecondeditionofthistext;andchemicalengineeringandtechnologyandengineeringeducationatBrighamYoungUniversity,wherehecowrotethe thirdeditionofthistext.Hereceivedteachingawardsatallthreeuniversitiesandservedasacting departmentchair,asassociatedean,andinBrighamYoungUniversity’scentraladministrationas anassociateintheOfficeofPlanningandAssessment.HeispastpresidentoftheRockyMountain sectionoftheAmericanSocietyforEngineeringEducation.HecurrentlyservesastheTechnology andEngineeringEducationprogramchairatBrighamYoungUniversity. J. Brandon RogersstudiedchemicalengineeringatBrighamYoungUniversity,wherehestudied reservoirengineeringusingthesecondeditionofthistext.Aftergraduation,heacceptedaposition atMurphyOilCorporationasaprojectengineer,duringwhichtimehecowrotethethirdedition ofthistext. xvii This page intentionally left blank Nomenclature Normal symbol Definition Units A arealextentofreservoirorwell acresorft2 Ac cross-sectionalareaperpendicularto fluidflow ft2 B′ waterinfluxconstant bbl/psia Bgi initialgasformationvolumefactor ft3/SCForbbl/SCF Bga gasformationvolumefactorat abandonmentpressure ft3/SCForbbl/SCF BIg formationvolumefactorofinjectedgas ft3/SCForbbl/SCF Bo oilformationvolumefactor bbl/STBorft3/STB Bofb oilformationvolumefactoratbubble pointfromseparatortest bbl/STBorft3/STB Boi oilformationvolumefactoratinitial reservoirpressure bbl/STBorft3/STB Bob oilformationvolumefactoratbubble pointpressure bbl/STBorft3/STB Bodb oilformationvolumefactoratbubble pointfromdifferentialtest bbl/STBorft3/STB Bt twophaseoilformationvolumefactor bbl/STBorft3/STB Bw waterformationvolumefactor bbl/STBorft3/STB c isothermalcompressibility psi–1 CA reservoirshapefactor unitless cf formationisothermalcompressibility psi–1 cg gasisothermalcompressibility psi–1 co oilisothermalcompressibility psi–1 cr reducedisothermalcompressibility fraction,unitless ct totalcompressibility psi–1 xix xx Nomenclature Normal symbol Definition Units cti totalcompressibilityatinitialreservoir pressure psi–1 cw waterisothermalcompressibility psi–1 E overallrecoveryefficiency fraction,unitless Ed microscopicdisplacementefficiency fraction,unitless Ei verticaldisplacementefficiency fraction,unitless Eo expansionofoil(HavlenaandOdeh method) bbl/STB Ef,w expansionofformationandwater (HavlenaandOdehmethod) bbl/STB Eg expansionofgas(HavlenaandOdeh method) bbl/STB Es arealdisplacementefficiency fraction,unitless Ev macroscopicorvolumetricdisplacement fraction,unitless efficiency fg gascutofreservoirfluidflow fraction,unitless fw watercutofreservoirfluidflow fraction,unitless F netproductionfromreservoir(Havlena andOdehmethod) bbl Fk ratioofverticaltohorizontal permeability unitless G initialreservoirgasvolume SCF Ga remaininggasvolumeatabandonment pressure SCF Gf volumeoffreegasinreservoir SCF G1 volumeofinjectedgas SCF Gps gasfromprimaryseparator SCF Gss gasfromsecondaryseparator SCF Gst gasfromstocktank SCF GE gasequivalentofoneSTBofcondensate SCF liquid GEw gasequivalentofoneSTBofproduced water SCF GOR gas-oilratio SCF/STB h formationthickness ft Nomenclature xxi Normal symbol Definition Units I injectivityindex STB/day-psi J productivityindex STB/day-psi Js specificproductivityindex STB/day-psi-ft Jsw productivityindexforastandardwell STB/day-psi k permeability md k′ waterinfluxconstant bbl/day-psia kavg averagepermeability md kg permeabilitytogasphase md ko permeabilitytooilphase md kw permeabilitytowaterphase md krg relativepermeabilitytogasphase fraction,unitless kro relativepermeabilitytooilphase fraction,unitless krw relativepermeabilitytowaterphase fraction,unitless L lengthoflinearflowregion ft m ratioofinitialreservoirfreegasvolume toinitialreservoiroilvolume ratio,unitless m(p) realgaspseudopressure psia2/cp m(pi) realgaspseudopressureatinitial reservoirpressure psia2/cp m(pwf) realgaspseudopressure,flowingwell psia2/cp M mobilityratio ratio,unitless Mw molecularweight lb/lb-mol Mwo molecularweightofoil lb/lb-mol n moles mol N initialvolumeofoilinreservoir STB Np cumulativeproducedoil STB Nvc capillarynumber ratio,unitless p pressure psia pb pressureatbubblepoint psia pc pressureatcriticalpoint psia Pc capillarypressure psia xxii Nomenclature Normal symbol Definition Units pD dimensionlesspressure ratio,unitless pe pressureatouterboundary psia pi pressureatinitialreservoirpressure psia p1hr pressureat1hourfromtransienttime periodonsemilogplot psia ppc pseudocriticalpressure psia ppr reducedpressure ratio,unitless pR pressureatareferencepoint psia psc pressureatstandardconditions psia pw pressureatwellboreradius psia pwf pressureatwellboreforflowingwell psia pwf ( Δt =0 ) pressureofflowingwelljustpriorto shutinforapressurebuilduptest psia pws shutinpressureatwellbore psia p volumetricaveragereservoirpressure psia Δp changeinvolumetricaveragereservoir pressure psia q flowrateinstandardconditionsunits bbl/day q′t totalflowrateinreservoirinreservoir volumeunits bbl/day r distancefromcenterofwell(radial dimension) ft rD dimensionlessradius ratio,unitless re distancefromcenterofwelltoouter boundary ft rR distancefromcenterofwelltooil reservoir ft rw distancefromcenterofwellbore ft R instantaneousproducedgas-oilratio SCF/STB R′ universalgasconstant Rp cumulativeproducedgas-oilratio SCF/STB Rso solutiongas-oilratio SCF/STB Nomenclature xxiii Normal symbol Definition Units Rsob solutiongas-oilratioatbubblepoint pressure SCF/STB Rsod solutiongas-oilratiofromdifferential liberationtest SCF/STB Rsodb solutiongas-oilratio,sumofoperator gas,andstock-tankgasfromseparator test SCF/STB Rsofb solutiongas-oilratio,sumofseparator gas,andstock-tankgasfromseparator test SCF/STB Rsoi solutiongas-oilratioatinitialreservoir pressure SCF/STB Rsw solutiongas-waterratioforbrine SCF/STB Rswp solutiongas-waterratiofordeionized water SCF/STB R1 solutiongas-oilratioforliquidstream outofseparator SCF/STB R3 solutiongas-oilratioforliquidstream outofstocktank SCF/STB RF recoveryfactor fraction,unitless R.V. relativevolumefromaflashliberation test ratio,unitless S fluidsaturation fraction,unitless Sg gassaturation fraction,unitless Sgr residualgassaturation fraction,unitless SL totalliquidsaturation fraction,unitless So oilsaturation fraction,unitless Sw watersaturation fraction,unitless Swi watersaturationatinitialreservoir conditions fraction,unitless t time hour Δt timeoftransienttest hour to dimensionlesstime ratio,unitless tp timeofconstantrateproductionpriorto hour wellshut-in xxiv Nomenclature Normal symbol Definition Units tpss timetoreachpseudosteadystateflow region hour T temperature °For°R Tc temperatureatcriticalpoint °For°R Tpc pseudocriticaltemperature °For°R Tpr reducedtemperature fraction,unitless Tppr pseudoreducedtemperature fraction,unitless Tsc temperatureatstandardconditions °For°R V volume ft3 Vb bulkvolumeofreservoir ft3oracre-ft Vp porevolumeofreservoir ft3 Vr relativeoilvolume ft3 VR gasvolumeatsomereferencepoint ft3 W widthoffracture ft Wp waterinflux bbl WeD dimensionlesswaterinflux ratio,unitless Wei encroachablewaterinplaceatinitial reservoirconditions bbl WI volumeofinjectedwater STB Wp cumulativeproducedwater STB z gasdeviationfactororgas compressibilityfactor ratio,unitless zi gasdeviationfactoratinitialreservoir pressure ratio,unitless Greek symbol Definition Units α dip angle degrees φ porosity fraction,unitless γ specificgravity ratio,unitless γg gasspecificgravity ratio,unitless γo oilspecificgravity ratio,unitless γw wellfluidspecificgravity ratio,unitless Nomenclature xxv Greek symbol Definition Units γ′ fluidspecificgravity(alwaysrelativeto water) ratio,unitless γ1 specificgravityofgascomingfrom separator ratio,unitless γ3 specificgravityofgascomingfrom stocktank ratio,unitless η formationdiffusivity ratio,unitless λ mobility(ratioofpermeabilityto viscosity) md/cp λg mobilityofgasphase md/cp λo mobilityofoilphase md/cp λw mobilityofwaterphase md/cp μ viscosity cp μg gasviscosity cp μi viscosityatinitialreservoirpressure cp μo oilviscosity cp μob oilviscosityatbubblepoint cp μod deadoilviscosity cp μw waterviscosity cp μw1 waterviscosityat14.7psiaandreservoir cp temperature μ1 viscosityat14.7psiaandreservoir temperature cp ν apparentfluidvelocityinreservoir bbl/day-ft2 νg apparentgasvelocityinreservoir bbl/day-ft2 νt apparenttotalvelocityinreservoir bbl/day-ft2 θ contactangle degrees ρ density lb/ft3 ρg gasdensity lb/ft3 ρr reduceddensity ratio,unitless ρo,API oildensity °API σwo oil-brineinterfacialtension dynes/cm This page intentionally left blank C H A P T E R 1 Introduction to Petroleum Reservoirs and Reservoir Engineering Whilethemodernpetroleumindustryiscommonlysaidtohavestartedin1859withCol.Edwin A.Drake’sfindinTitusville,Pennsylvania,recordedhistoryindicatesthattheoilindustrybegan atleast6000yearsago.Thefirstoilproductswereusedmedicinally,assealants,asmortar,aslubricants,andforillumination.Drake’sfindrepresentedthebeginningofthemodernera;itwasthe firstrecordedcommercialagreementtodrillfortheexclusivepurposeoffindingpetroleum.While thewellhedrilledwasnotcommerciallysuccessful,itdidbeginthepetroleumerabyleadingtoan intenseinterestinthecommercialproductionofpetroleum.Thepetroleumerahadbegun,andwith itcametheriseofpetroleumgeologyandreservoirengineering. 1.1 Introduction to Petroleum Reservoirs Oilandgasaccumulationsoccurinundergroundtrapsformedbystructuraland/orstratigraphicfeatures.1*Figure1.1isaschematicrepresentationofastratigraphictrap.Fortunately,thehydrocarbon accumulationsusuallyoccurinthemoreporousandpermeableportionofbeds,whicharemainly sands,sandstones,limestones,anddolomites;intheintergranularopenings;orinporespacescaused byjoints,fractures,andsolutionactivity.Areservoiristhatportionofthetrappedformationthatcontainsoiland/orgasasasinglehydraulicallyconnectedsystem.Insomecasestheentiretrapisfilled withoilorgas,andintheseinstancesthetrapandthereservoirarethesame.Oftenthehydrocarbon reservoirishydraulicallyconnectedtoavolumeofwater-bearingrockcalledanaquifer.Manyreservoirsarelocatedinlargesedimentarybasinsandshareacommonaquifer.Whenthisoccurs,the productionoffluidfromonereservoirwillcausethepressuretodeclineinotherreservoirsbyfluid communicationthroughtheaquifer. Hydrocarbonfluidsaremixturesofmoleculescontainingcarbonandhydrogen.Underinitialreservoirconditions,thehydrocarbonfluidsareineitherasingle-phaseoratwo-phasestate. * Referencesthroughoutthetextaregivenattheendofeachchapter. 1 2 Chapter 1 • Introduction to Petroleum Reservoirs and Reservoir Engineering Porous channel sandstone Gas Oil Water Figure 1.1 Impermeable shale Schematic representation of a hydrocarbon deposit in a stratigraphic trap. Asingle-phasereservoirfluidmaybeinaliquidphase(oil)oragasphase(naturalgas).Ineither case, when produced to the surface, most hydrocarbon fluids will separate into gas and liquid phases.Gasproducedatthesurfacefromafluidthatisliquidinthereservoiriscalleddissolved gas.Therefore,avolumeofreservoiroilwillproducebothoilandtheassociateddissolvedgasat thesurface,andbothdissolvednaturalgasandcrudeoilvolumesmustbeestimated.Ontheother hand,liquidproducedatthesurfacefromafluidthatisgasinthereservoiriscalledgas condensatebecausetheliquidcondensesfromthegasphase.Anoldernameforgascondensateisgas distillate.Inthiscase,avolumeofreservoirgaswillproducebothnaturalgasandcondensateat thesurface,andbothgasandcondensatevolumesmustbeestimated.Wherethehydrocarbonaccumulationisinatwo-phasestate,theoverlyingvaporphaseiscalledthegas capandtheunderlying liquidphaseiscalledtheoil zone.Therewillbefourtypesofhydrocarbonvolumestobeestimated whenthisoccurs:thefreegasorassociatedgas,thedissolvedgas,theoilintheoilzone,andthe recoverablenaturalgasliquid(condensate)fromthegascap. Although the hydrocarbons in place are fixed quantities, which are referred to as the resource,thereservesdependonthemechanismsbywhichthereservoirisproduced.Inthemid1930s, theAmerican Petroleum Institute (API) created a definition for reserves. Over the next severaldecades,otherinstitutions,includingtheAmericanGasAssociation(AGA),theSecurities andExchangeCommissions(SEC),theSocietyofPetroleumEngineers(SPE),theWorldPetroleumCongress(nowCouncil;WPC),andtheSocietyofPetroleumEvaluationEngineers(SPEE), haveallbeenpartofcreatingformaldefinitionsofreservesandotherrelatedterms.Recently,the SPEcollaboratedwiththeWPC,theAmericanAssociationofPetroleumGeologists(AAPG),and theSPEEtopublishthePetroleumResourcesManagementSystem(PRMS).2SomeofthedefinitionsusedinthePRMSpublicationarepresentedinTable1.1.Theamountsofoilandgasinthese definitionsarecalculatedfromavailableengineeringandgeologicdata.Theestimatesareupdated overtheproducinglifeofthereservoirasmoredatabecomeavailable.ThePRMSdefinitionsare obviouslyfairlycomplicatedandincludemanyotherfactorsthatarenotdiscussedinthistext.For moredetailedinformationregardingthesedefinitions,thereaderisencouragedtoobtainacopyof thereference. 1.1 Introduction to Petroleum Reservoirs 3 Table 1.1 Definitions of Petroleum Terms from the Petroleum Resources Management System2 Petroleumisdefinedasanaturallyoccurringmixtureconsistingofhydrocarbonsinthegaseous,liquid,or solidphase.Petroleummayalsocontainnonhydrocarbons,commonexamplesofwhicharecarbondioxide, nitrogen,hydrogensulfide,andsulfur.Inrarecases,nonhydrocarboncontentcouldbegreaterthan50%. The term resources as used herein is intended to encompass all quantities of petroleum naturally occurring on or within the Earth’s crust, discovered and undiscovered (recoverable and unrecoverable), plus thosequantitiesalreadyproduced.Further,itincludesalltypesofpetroleum,whethercurrentlyconsidered “conventional”or“unconventional.” Total petroleum initially-in-placeisthatquantityofpetroleumthatisestimatedtoexistoriginallyinnaturallyoccurringaccumulations.Itincludesthatquantityofpetroleumthatisestimated,asofagivendate,tobecontainedinknownaccumulationspriortoproduction,plusthose estimatedquantitiesinaccumulationsyettobediscovered(equivalentto“totalresources”). Discovered petroleum initially-in-placeisthatquantityofpetroleumthatisestimated,asofa givendate,tobecontainedinknownaccumulationspriortoproduction. Production is the cumulative quantity of petroleum that has been recovered at a given date. Whileallrecoverableresourcesareestimatedandproductionismeasuredintermsofthesales productspecifications,rawproduction(salesplusnonsales)quantitiesarealsomeasuredand requiredtosupportengineeringanalysesbasedonreservoirvoidage.Multipledevelopment projectsmaybeappliedtoeachknownaccumulation,andeachprojectwillrecoveranestimatedportionoftheinitially-in-placequantities.Theprojectsaresubdividedintocommercial and subcommercial,withtheestimatedrecoverablequantitiesbeingclassifiedasreservesand contingentresources,respectively,whicharedefinedasfollows. Reservesarethosequantitiesofpetroleumanticipatedtobecommerciallyrecoverablebyapplicationofdevelopmentprojectstoknownaccumulationsfromagivendateforwardunder definedconditions.Reservesmustfurthersatisfyfourcriteria:theymustbediscovered,recoverable,commercial,andremaining(asoftheevaluationdate),basedonthedevelopment project(s)applied.Reservesarefurthercategorizedinaccordancewiththelevelofcertainty associatedwiththeestimatesandmaybesubclassifiedbasedonprojectmaturityand/orcharacterizedbydevelopmentandproductionstatus. Contingent resourcesarethosequantitiesofpetroleumestimated,asofagivendate,tobepotentiallyrecoverablefromknownaccumulations,buttheappliedproject(s)arenotyetconsidered matureenoughforcommercialdevelopmentduetooneormorecontingencies.Contingent resourcesmayinclude,forexample,projectsforwhichtherearecurrentlynoviablemarkets, wherecommercialrecoveryisdependentontechnologyunderdevelopmentorwhereevaluationoftheaccumulationisinsufficienttoclearlyassesscommerciality.Contingentresources arefurthercategorizedinaccordancewiththelevelofcertaintyassociatedwiththeestimates andmaybesubclassifiedbasedonprojectmaturityand/orcharacterizedbytheireconomic status. Undiscovered petroleum initially-in-placeisthatquantityofpetroleumestimated,asofagiven date,tobecontainedwithinaccumulationsyettobediscovered. Prospective resourcesarethosequantitiesofpetroleumestimated,asofagivendate,tobepotentiallyrecoverablefromundiscoveredaccumulationsbyapplicationoffuturedevelopment projects.Prospectiveresourceshavebothanassociatedchanceofdiscoveryandachanceof development. Prospective resources are further subdivided in accordance with the level of certaintyassociatedwithrecoverableestimates,assumingtheirdiscoveryanddevelopment andmaybesubclassifiedbasedonprojectmaturity. (continued) 4 Chapter 1 • Introduction to Petroleum Reservoirs and Reservoir Engineering Table 1.1 Definitions of Petroleum Terms from the Petroleum Resources Management System2 (continued) Unrecoverablereferstotheportionofdiscoveredorundiscoveredpetroleuminitially-in-place quantitiesthatisestimated,asofagivendate,nottoberecoverablebyfuturedevelopment projects.Aportionofthesequantitiesmaybecomerecoverableinthefutureascommercial circumstanceschangeortechnologicaldevelopmentsoccur;theremainingportionmaynever be recovered due to physical/chemical constraints represented by subsurface interaction of fluidsandreservoirrocks. Further,estimated ultimate recovery (EUR) isnotaresourcescategorybutatermthatmaybeappliedto anyaccumulationorgroupofaccumulations(discoveredorundiscovered)todefinethosequantitiesofpetroleumestimated,asofagivendate,tobepotentiallyrecoverableunderdefinedtechnicalandcommercial conditionsplusthosequantitiesalreadyproduced(totalofrecoverableresources). Inspecializedareas,suchasbasinpotentialstudies,alternativeterminologyhasbeenused;thetotalresourcesmaybereferredtoastotal resource base or hydrocarbon endowment.TotalrecoverableorEURmay betermedbasin potential.Thesumofreserves,contingentresources,andprospectiveresourcesmaybereferredtoasremaining recoverable resources.Whensuchtermsareused,itisimportantthateachclassification componentofthesummationalsobeprovided.Moreover,thesequantitiesshouldnotbeaggregatedwithout dueconsiderationofthevaryingdegreesoftechnicalandcommercialriskinvolvedwiththeirclassification. 1.2 History of Reservoir Engineering Crudeoil,naturalgas,andwaterarethesubstancesthatareofchiefconcerntopetroleumengineers.Althoughthesesubstancescanoccurassolidsorsemisolidssuchasparaffin,asphaltine, orgas-hydrate,usuallyatlowertemperaturesandpressures,inthereservoirandinthewells, theyoccurmainlyasfluids,eitherinthevapor(gaseous)orintheliquidphaseor,quitecommonly,both.Evenwheresolidmaterialsareused,asindrilling,cementing,andfracturing,theyare handledasfluidsorslurries.Theseparationofwellorreservoirfluidintoliquidandgas(vapor) phasesdependsmainlyontemperature,pressure,andthefluidcomposition.Thestateorphase ofafluidinthereservoirusuallychangeswithdecreasingpressureasthereservoirfluidisbeing produced.The temperature in the reservoir stays relatively constant during the production. In manycases,thestateorphaseinthereservoirisquiteunrelatedtothestateofthefluidwhenit isproducedatthesurface,duetochangesinbothpressureandtemperatureasthefluidrisesto thesurface.Thepreciseknowledgeofthebehaviorofcrudeoil,naturalgas,andwater,singlyor incombination,understaticconditionsorinmotioninthereservoirrockandinpipesandunder changingtemperatureandpressure,isthemainconcernofreservoirengineers. Asearlyas1928,reservoirengineersweregivingseriousconsiderationtogas-energyrelationships and recognized the need for more precise information concerning physical conditions inwellsandundergroundreservoirs.Earlyprogressinoilrecoverymethodsmadeitobviousthat computations made from wellhead or surface data were generally misleading. Sclater and Stephensondescribedthefirstrecordingbottom-holepressuregaugeandamechanismforsampling fluids under pressure in wells.3 It is interesting that this reference defines bottom-hole data as 1.2 History of Reservoir Engineering 5 measurementsofpressure,temperature,gas-oilratio,andthephysicalandchemicalnaturesofthe fluids.Theneedforaccuratebottom-holepressureswasfurtheremphasizedwhenMillikanand Sidwelldescribedthefirstprecisionpressuregaugeandpointedoutthefundamentalimportanceof bottom-holepressurestoreservoirengineersindeterminingthemostefficientoilrecoverymethods andliftingprocedures.4Withthiscontribution,theengineerwasabletomeasurethemostimportantbasicdataforreservoirperformancecalculations:reservoir pressure. Thestudyofthepropertiesofrocksandtheirrelationshiptothefluidstheycontaininboth the static and flowing states is called petrophysics. Porosity, permeability, fluid saturations and distributions,electricalconductivityofboththerockandthefluids,porestructure,andradioactivityaresomeofthemoreimportantpetrophysicalpropertiesofrocks.Fancher,Lewis,andBarnes madeoneoftheearliestpetrophysicalstudiesofreservoirrocksin1933,andin1934,Wycoff, Botset,Muskat,andReeddevelopedamethodformeasuringthepermeabilityofreservoirrock samplesbasedonthefluidflowequationdiscoveredbyDarcyin1856.5,6WycoffandBotsetmade asignificantadvanceintheirstudiesofthesimultaneousflowofoilandwaterandofgasandwater inunconsolidatedsands.7Thisworkwaslaterextendedtoconsolidatedsandsandotherrocks,and in1940LeverettandLewisreportedresearchonthethree-phaseflowofoil,gas,andwater.8 Itwasrecognizedbythepioneersinreservoirengineeringthatbeforereservoirvolumesofoil andgasinplacecouldbecalculated,thechangeinthephysicalpropertiesofbottom-holesamplesof thereservoirfluidswithpressurewouldberequired.Accordingly,in1935,Schilthuisdescribedabottom-holesamplerandamethodofmeasuringthephysicalpropertiesofthesamplesobtained.9These measurements included the pressure-volume-temperature relations, the saturation or bubble-point pressure,thetotalquantityofgasdissolvedintheoil,thequantitiesofgasliberatedundervarious conditionsoftemperatureandpressure,andtheshrinkageoftheoilresultingfromthereleaseofits dissolvedgasfromsolution.Thesedataenabledthedevelopmentofcertainusefulequations,andthey alsoprovidedanessentialcorrectiontothevolumetricequationforcalculatingoilinplace. The next significant development was the recognition and measurement of connate water saturation,whichwasconsideredindigenoustotheformationandremainedtooccupyapartofthe porespaceafteroilorgasaccumulation.10,11Thisdevelopmentfurtherexplainedthepooroiland gasrecoveriesinlowpermeabilitysandswithhighconnatewatersaturationandintroducedthe conceptofwater,oil,andgassaturationsaspercentagesofthetotalporespace.Themeasurement ofwatersaturationprovidedanotherimportantcorrectiontothevolumetricequationbyconsideringthehydrocarbonporespaceasafractionofthetotalporevolume. Althoughtemperatureandgeothermalgradientshadbeenofinteresttogeologistsformany years,engineerscouldnotmakeuseoftheseimportantdatauntilaprecisionsubsurfacerecording thermometer was developed. Millikan pointed out the significance of temperature data in applicationstoreservoirandwellstudies.12Fromthesebasicdata,Schilthuiswasabletoderive ausefulequation,commonlycalledtheSchilthuismaterialbalanceequation.13Amodification ofanearlierequationpresentedbyColeman,Wilde,andMoore,theSchilthuisequationisone ofthemostimportanttoolsofreservoirengineers.14Itisastatementoftheconservationofmatterandisamethodofaccountingforthevolumesandquantitiesoffluidsinitiallypresentin, producedfrom,injectedinto,andremaininginareservoiratanystageofdepletion.Odehand 6 Chapter 1 • Introduction to Petroleum Reservoirs and Reservoir Engineering Havlenahaveshownhowthematerialbalanceequationcanbearrangedintoaformofastraight line and solved.15 When production of oil or gas underlain by a much larger aquifer volume causes the waterintheaquifertoriseorencroachintothehydrocarbonreservoir,thereservoirissaidto beunderwaterdrive.Inreservoirsunderwaterdrive,thevolumeofwaterencroachinginto thereservoirisalsoincludedmathematicallyinthematerialbalanceonthefluids.Although Schilthuisproposedamethodofcalculatingwaterencroachmentusingthematerial-balance equation,itremainedforHurstand,later,vanEverdingenandHursttodevelopmethodsfor calculatingwaterencroachmentindependentofthematerialbalanceequation,whichapplyto aquifersofeitherlimitedorinfiniteextent,ineithersteady-stateorunsteady-stateflow.13,16,17 ThecalculationsofvanEverdingenandHursthavebeensimplifiedbyFetkovich.18Following thesedevelopmentsforcalculatingthequantitiesofoilandgasinitiallyinplaceoratanystage ofdepletion,TarnerandBuckleyandLeverettlaidthebasisforcalculatingtheoilrecovery tobeexpectedforparticularrockandfluidcharacteristics.19,20Tarnerand,later,Muskat21 presentedmethodsforcalculatingrecoverybytheinternalorsolutiongasdrivemechanism,and BuckleyandLeverett20presentedmethodsforcalculatingthedisplacementofoilbyexternal gascapdriveandwaterdrive.Thesemethodsnotonlyprovidedmeansforestimatingrecoveriesforeconomicstudies;theyalsoexplainedthecausefordisappointinglylowrecoveriesin manyfields.Thisdiscoveryinturnpointedthewaytoimprovedrecoveriesbytakingadvantageofthenaturalforcesandenergies,bysupplyingsupplementalenergybygasandwater injection,andbyunitizingreservoirstooffsetthelossesthatmaybecausedbycompetitive operations. Duringthe1960s,thetermsreservoir simulation and reservoir mathematical modelingbecamepopular.22–24Thesetermsaresynonymousandrefertotheabilitytousemathematicalformulastopredicttheperformanceofanoilorgasreservoir.Reservoirsimulationwasaidedbythe developmentoflarge-scale,high-speeddigitalcomputers.Sophisticatednumericalmethodswere alsodevelopedtoallowthesolutionofalargenumberofequationsbyfinite-differenceorfiniteelementtechniques. Withthedevelopmentofthesetechniques,concepts,andequations,reservoirengineering becameapowerfulandwell-definedbranchofpetroleumengineering.Reservoir engineeringmay bedefinedastheapplicationofscientificprinciplestothedrainageproblemsarisingduringthe developmentandproductionofoilandgasreservoirs.Ithasalsobeendefinedas“theartofdevelopingandproducingoilandgasfluidsinsuchamannerastoobtainahigheconomicrecovery.”25 Theworkingtoolsofthereservoirengineeraresubsurfacegeology,appliedmathematics,andthe basiclawsofphysicsandchemistrygoverningthebehaviorofliquidandvaporphasesofcrude oil,naturalgas,andwaterinreservoirrocks.Becausereservoirengineeringisthescienceofproducingoilandgas,itincludesastudyofallthefactorsaffectingtheirrecovery.ClarkandWessely urgedajointapplicationofgeologicalandengineeringdatatoarriveatsoundfielddevelopment programs.26Ultimately,reservoirengineeringconcernsallpetroleumengineers,fromthedrilling engineerwhoisplanningthemudprogram,tothecorrosionengineerwhomustdesignthetubing stringfortheproducinglifeofthewell. 1.3 1.3 Introduction to Terminology 7 Introduction to Terminology Thepurposeofthissectionistoprovideanexplanationtothereaderoftheterminologythatwillbe usedthroughoutthebookbyprovidingcontextforthetermsandexplainingtheinteractionofthe terms.Beforedefiningtheseterms,noteFig.1.2,whichillustratesacrosssectionofaproducing petroleumreservoir. Areservoirisnotanopenundergroundcavernfullofoilandgas.Rather,itissectionof porousrock(beneathanimperviouslayerofrock)thathascollectedhighconcentrationsofoiland gasintheminutevoidspacesthatweavethroughtherock.Thatoilandgas,alongwithsomewater, aretrappedbeneaththeimperviousrock.Thetermporosity(φ)isameasure,expressedinpercent, ofthevoidspaceintherockthatisfilledwiththereservoirfluid. Reservoirfluidsaresegregatedintophasesaccordingtothedensityofthefluid.Oilspecific gravity(γo)istheratioofthedensityofoiltothedensityofwater,andgasspecificgravity(γg)is theratioofthedensityofnaturalgastothedensityofair.Asthedensityofgasislessthanthat ofoilandbotharelessthanwater,gasrestsatthetopofthereservoir,followedbyoilandfinally water.Usuallytheinterfacebetweentworeservoirfluidphasesishorizontalandiscalledacontact. Betweengasandoilisagas-oilcontact,betweenoilandwaterisanoil-watercontact,andbetween gasandwaterisagas-watercontactifnooilphaseispresent.Asmallvolumeofwatercalledconnate(orinterstitial)waterremainsintheoilandgaszonesofthereservoir. Drilling rig Natural gas Earth’s crust Shale Impervious rock Petroleum Water Impervious rock Figure 1.2 Diagram to show the occurrence of petroleum under the Earth’s surface. 8 Chapter 1 • Introduction to Petroleum Reservoirs and Reservoir Engineering Theinitialamountoffluidinareservoirisextremelyimportant.Inpractice,thesymbolN (comingfromtheGreekwordnaptha)representstheinitialvolumeofoilinthereservoirexpressed asastandardsurfacevolume,suchasthestock-tankbarrel(STB).G and Wareinitialreservoir gasandwater,respectively.Asthesefluidsareproduced,thesubscriptpisaddedtoindicatethe cumulativeoil(Np),gas(Gp),orwater(Wp)produced. Thetotalreservoirvolumeisfixedanddependentontherockformationsofthearea.Asreservoirfluidisproducedandthereservoirpressuredrops,boththerockandthefluidremaininginthe reservoirexpand.If10%ofthefluidisproduced,theremaining90%inthereservoirmustexpand tofilltheentirereservoirvoidspace.Whenthehydrocarbonreservoirisincontactwithanaquifer, boththehydrocarbonfluidsandthewaterintheaquiferexpandashydrocarbonsareproduced,and waterenteringthehydrocarbonspacecanreplacethevolumeofproducedhydrocarbons. Toaccountforallthereservoirfluidaspressurechanges,avolumefactor(B)isused.The volumefactorisaratioofthevolumeofthefluidatreservoirconditionstoitsvolumeatatmosphericconditions(usually60°Fand14.7psi).Oilvolumeattheseatmosphericconditionsismeasured inSTBs(onebarrelisequalto42gallons).Producedgasesaremeasuredinstandardcubicfeet (SCF).AnM(1000)orMM(1million)orMMM(1billion)isfrequentlyplacedbeforetheunits SCF.Aslongasonlyliquidphasesareinthereservoir,theoilandwatervolumefactors(Bo and Bw)willbeginattheinitialoilvolumefactors(Boi and Bwi)andthensteadilyincreaseveryslightly (by1%–5%).Oncethesaturationpressureisreachedandgasstartsevolvingfromsolution,theoil volumefactorwilldecrease.Gas(Bg)volumefactorswillincreaseconsiderably(10-foldormore) asthereservoirpressuredrops.Thechangeinvolumefactorforameasuredchangeinthereservoir pressureallowsforsimpleestimationoftheinitialgasoroilvolume. Whenthewellfluidreachesthesurface,itisseparatedintogasandoil.Figure1.3showsa two-stageseparationsystemwithaprimaryseparatorandastocktank.Thewellfluidisintroduced intotheprimaryseparatorwheremostoftheproducedgasisobtained.Theliquidfromtheprimary separatoristhenflashedintothestocktank.TheliquidaccumulatedinthestocktankisNp , and any gasfromthestocktankisaddedtotheprimarygastoarriveatthetotalproducedsurfacegas,Gp. Atthispoint,theproducedamountsofoilandgasaremeasured,samplesaretaken,andthesedata areusedtoevaluateandforecasttheperformanceofthewell. Gps Well fluid Primary separator Gst Gp Stock tank Np Figure 1.3 Schematic representation of produced well fluid and a surface separator system. 1.4 Reservoir Types Defined with Reference to Phase Diagrams 9 1.4 Reservoir Types Defined with Reference to Phase Diagrams Fromatechnicalpointofview,thevarioustypesofreservoirscanbedefinedbythelocationofthe initialreservoirtemperatureandpressurewithrespecttothetwo-phase(gasandliquid)envelopeas commonlyshownonpressure-temperature(PT)phasediagrams.Figure1.4isthePTphasediagram foraparticularreservoirfluid.Theareaenclosedbythebubble-pointanddew-pointcurvesrepresents pressureandtemperaturecombinationsforwhichbothgasandliquidphasesexist.Thecurveswithin thetwo-phaseenvelopeshowthepercentageofthetotalhydrocarbonvolumethatisliquidforany temperatureandpressure.Atpressureandtemperaturepointslocatedabovethebubble-pointcurve, thehydrocarbonmixturewillbealiquidphase.Atpressureandtemperaturepointslocatedaboveor totherightofthedew-pointcurve,thehydrocarbonmixturewillbeagasphase.Thecriticalpoint, wherebubble-point,dew-point,andconstantqualitycurvesmeet,representsamathematicaldiscontinuity,andphasebehaviornearthispointisdifficulttodefine.Initially,eachhydrocarbonaccumulationwillhaveitsownphasediagram,whichdependsonlyonthecompositionoftheaccumulation. ConsiderareservoircontainingthefluidofFig.1.4initiallyat300°Fand3700psia,pointA. Sincethispointliesoutsidethetwo-phaseregionandtotherightofthecriticalpoint,thefluidisoriginallyinaone-phasegasstate.Sincethefluidremaininginthereservoirduringproductionremains at300°F,itisevidentthatitwillremaininthesingle-phaseorgaseousstateasthepressuredeclines alongpath AA1 . Furthermore,thecompositionoftheproducedwellfluidswillnotchangeasthe reservoirisdepleted.Thisistrueforanyaccumulationwiththishydrocarboncompositionwherethe reservoirtemperatureexceedsthecricondentherm,ormaximumtwo-phasetemperature(250°Ffor thepresentexample).Althoughthefluidleftinthereservoirremainsinonephase,thefluidproduced throughthewellboreandintosurfaceseparators,althoughthesamecomposition,mayenterthetwophaseregionowingtothetemperaturedecline,asalongline AA2 . Thisaccountsfortheproduction ofcondensateliquidatthesurfacefromasingle-phasegasphaseinthereservoir.Ofcourse,ifthe cricondenthermofafluidisbelowapproximately50°F,thenonlygaswillexistonthesurfaceatusualambienttemperatures,andtheproductionwillbecalleddry gas.Nevertheless,evendrygasmay containvaluableliquidfractionsthatcanberemovedbylow-temperatureseparation. Next, consider a reservoir containing the same fluid of Fig. 1.4 but at a temperature of 180°Fandaninitialpressureof3300psia,pointB.Herethefluidisalsoinitiallyintheonephase gas state, because the reservoir temperature exceeds the critical-point temperature.As pressuredeclinesduetoproduction,thecompositionoftheproducedfluidwillbethesameas reservoir Aandwillremainconstantuntilthedew-pointpressureisreachedat2700psia,point B1.Belowthispressure,aliquidcondensesoutofthereservoirfluidasafogordew.Thistype ofreservoiriscommonlycalledadew-pointoragas-condensatereservoir.Thiscondensation leavesthegasphasewithalowerliquidcontent.Thecondensedliquidremainsimmobileatlow concentrations.Thusthegasproducedatthesurfacewillhavealowerliquidcontent,andthe producinggas-oilratiothereforerises.Thisprocessofretrogradecondensationcontinuesuntila pointofmaximumliquidvolumeisreached,10%at2250psia,pointB2.Thetermretrograde is usedbecausegenerallyvaporization,ratherthancondensation,occursduringisothermalexpansion.Afterthedewpointisreached,becausethecompositionoftheproducedfluidchanges,the Chapter 1 10 • Introduction to Petroleum Reservoirs and Reservoir Engineering 4000 Reservoir pressure, psia B1 2500 t in De w C1 po in o p le bb Bu t B2 % 80 D 2000 % 40 % 20 1500 e 10 l vo 5% d ui A1 0% 1000 A2 500 Figure 1.4 on % um Liq ducti Critical point C Path of reservoir fluid 3000 B Single-phase gas reservoirs A f pro TC = 127ºF 3500 Cricondentherm = 250ºF Dew point or retrograde gas–condensate reservoirs Path o Bubble point or dissolved gas reservoirs 0 50 100 B3 150 200 Reservoir temperature, ºF 250 300 350 Pressure-temperature phase diagram of a reservoir fluid. compositionoftheremainingreservoirfluidalsochanges,andthephaseenvelopebeginstoshift. ThephasediagramofFig.1.4representsoneandonlyonehydrocarbonmixture.Unfortunately, thisshiftistowardtherightandfurtheraggravatestheretrogradeliquidlosswithintheporesof thereservoirrock. Neglectingforthemomentthisshiftinthephasediagram,forqualitativepurposes,vaporizationoftheretrogradeliquidoccursfromB2totheabandonmentpressureB3.Thisrevaporizationaids liquidrecoveryandmaybeevidencedbydecreasinggas-oilratiosonthesurface.Theoverallretrogradelosswillevidentlybegreater(1)forlowerreservoirtemperatures,(2)forhigherabandonment pressures,and(3)forgreatershiftofthephasediagramtotheright—thelatterbeingapropertyof thehydrocarbonsystem.Theretrogradeliquidinthereservoiratanytimeiscomposedofmostly methaneandethanebyvolume,andsoitismuchlargerthanthevolumeofstableliquidthatcouldbe 1.4 Reservoir Types Defined with Reference to Phase Diagrams 11 obtainedfromitatatmospherictemperatureandpressure.Thecompositionofthisretrogradeliquid ischangingaspressuredeclinessothat4%retrogradeliquidvolumeat,forexample,750psiamight containasmuchsurfacecondensateas6%retrogradeliquidvolumeat2250psia. Iftheinitialreservoirfluidcompositionisfoundat2900psiaand75°F,pointC,thereservoir wouldbeinaone-phasestate,nowcalledliquid,becausethetemperatureisbelowthecritical-point temperature.Thisiscalledabubble-point(orblack-oilorsolution-gas)reservoir.Aspressuredeclinesduringproduction,thebubble-pointpressurewillbereached,inthiscaseat2550psia,point C1.Belowthispressure,bubbles,orafree-gasphase,willappear.Whenthefreegassaturationis sufficientlylarge,gasflowstothewellboreineverincreasingquantities.Becausesurfacefacilities limitthegasproductionrate,theoilflowratedeclines,andwhentheoilrateisnolongereconomic, muchunrecoveredoilremainsinthereservoir. Finally,iftheinitialhydrocarbonmixtureoccurredat2000psiaand150°F,pointD,it wouldbeatwo-phasereservoir,consistingofaliquidoroilzoneoverlainbyagaszoneorcap. Becausethecompositionofthegasandoilzonesareentirelydifferentfromeachother,they may be represented separately by individual phase diagrams that bear little relation to each otherortothecomposite.Theliquidoroilzonewillbeatitsbubblepointandwillbeproduced asabubble-pointreservoirmodifiedbythepresenceofthegascap.Thegascapwillbeatthe dewpointandmaybeeitherretrograde,asshowninFig.1.5(a),ornonretrograde,asshownin Fig.1.5(b). Fromthistechnicalpointofview,hydrocarbonreservoirsareinitiallyeitherinasingle-phase state(A, B, or C)orinatwo-phasestate(D),dependingontheirtemperaturesandpressuresrelative totheirphaseenvelopes.Table1.2depictsasummaryofthesefourtypes.Thesereservoirtypesare discussedindetailinChapters4,5,6,and7,respectively. c c Gas Oil P Gas BP P Pressure c BP Pressure BP BP T Temperature (a) Figure 1.5 DP DP DP Oil DP c T Temperature (b) Phase diagrams of a cap gas and oil zone fluid showing (a) retrograde cap gas and (b) nonretrograde cap gas. 12 Chapter 1 • Introduction to Petroleum Reservoirs and Reservoir Engineering Table 1.2 Summary of Reservoir Types Type A single phase gas Type B gas condensate Type C undersaturated oil Typical primary recovery mechanism Volumetricgas drive Volumetricgas drive Depletiondrive, Volumetricgasdrive, waterdrive depletiondrive, waterdrive Initial reservoir conditions Singlephase:Gas Singlephase:Gas Singlephase:Oil Reservoirfluid remainsasgas. Liquidcondenses inthereservoir. Gasvaporizesin Saturatedoilreleases reservoir. additionalgas. Primarilygas Gasand condensate Reservoir behavior as pressure declines Produced hydrocarbons Oil and gas Type D saturated oil Twophase: Oil and gas Oil and gas Table1.3presentsthemolecompositionsandsomeadditionalpropertiesoffivesingle-phase reservoirfluids.Thevolatileoilisintermediatebetweenthegascondensateandtheblack,orheavy, oiltypes.Productionwithgas-oilratiosgreaterthan100,000SCF/STBiscommonlycalledlean or dry gas,althoughthereisnogenerallyrecognizeddividinglinebetweenthetwocategories.In somelegalwork,statutorygaswellsarethosewithgas-oilratiosinexcessof100,000SCF/STB. Thetermwet gasissometimesusedinterchangeablywithgas condensate.Inthegas-oilratios, generaltrendsarenoticeableinthemethaneandheptanes-pluscontentofthefluidsandthecolorof thetankliquids.Althoughthereisgoodcorrelationbetweenthemolecularweightoftheheptanes plusandthegravityofthestock-tankliquid,thereisvirtuallynocorrelationbetweenthegas-oil ratiosandthegravitiesofthestock-tankliquids,exceptthatmostblackoilreservoirshavegas-oil ratiosbelow1000SCF/STBandstock-tankliquidgravitiesbelow45°API.Thegas-oilratiosare agoodindicationoftheoverallcompositionofthefluid,highgas-oilratiosbeingassociatedwith lowconcentrationsofpentanesandheavierandviceversa. Thegas-oilratiosgiveninTable1.3arefortheinitialproductionoftheone-phasereservoir fluids producing through one or more surface separators operating at various temperatures and pressures,whichmayvaryconsiderablyamongtheseveraltypesofproduction.Thegas-oilratios andconsequentlytheAPIgravityoftheproducedliquidvarywiththenumber,pressures,andtemperaturesoftheseparatorssothatoneoperatormayreportasomewhatdifferentgas-oilratiofrom another,althoughbothproducethesamereservoirfluid.Also,aspressuredeclinesintheblackoil, volatileoil,andsomegas-condensatereservoirs,thereisgenerallyaconsiderableincreaseinthe gas-oilratioowingtothereservoirmechanismsthatcontroltherelativeflowofoilandgastothe wellbores.Theseparatorefficienciesalsogenerallydeclineasflowingwellheadpressuresdecline, whichalsocontributestoincreasedgas-oilratios. Whathasbeensaidpreviouslyappliestoreservoirsinitiallyinasinglephase.Theinitialgasoilratioofproductionfromwellscompletedeitherinthegascaporintheoilzoneoftwo-phase reservoirsdepends,asdiscussedpreviously,onthecompositionsofthegascaphydrocarbonsand theoilzonehydrocarbons,aswellasthereservoirtemperatureandpressure.Thegascapmaycontaingascondensateordrygas,whereastheoilzonemaycontainblackoilorvolatileoil.Naturally, 1.5 Production from Petroleum Reservoirs 13 Table 1.3 Mole Composition and Other Properties of Typical Single-Phase Reservoir Fluids Component Black oil Volatile oil Gas condensate Dry gas Wet gas C1 48.83 64.36 87.07 95.85 86.67 C2 2.75 7.52 4.39 2.67 7.77 C3 1.93 4.74 2.29 0.34 2.95 C4 1.60 4.12 1.74 0.52 1.73 C5 1.15 2.97 0.83 0.08 0.88 C6 1.59 1.38 0.60 0.12 C7+ 42.15 14.91 3.80 0.42 Total 100.00 100.00 100.00 100.00 Mol.wt.C7+ 225 181 112 157 GOR,SCF/ STB 625 2000 18,200 105,000 Tankgravity, °API 34.3 50.1 60.8 54.7 Liquidcolor Greenish black Mediumorange Lightstraw Waterwhite 100.00 Infinite ifawelliscompletedinboththegasandoilzones,theproductionwillbeamixtureofthetwo. Sometimesthisisunavoidable,aswhenthegasandoilzones(columns)areonlyafewfeetin thickness.Evenwhenawelliscompletedintheoilzoneonly,thedownwardconingofgasfrom theoverlyinggascapmayoccurtoincreasethegas-oilratiooftheproduction. 1.5 Production from Petroleum Reservoirs Productionfrompetroleumreservoirsisareplacementprocess.Thismeansthatwhenhydrocarbon isproducedfromareservoir,thespacethatitoccupiedmustbereplacedwithsomething.That somethingcouldbetheswellingoftheremaininghydrocarbonduetoadropinreservoirpressure, theencroachmentofwaterfromaneighboringaquifer,ortheexpansionofformation. Theinitialproductionofhydrocarbonsfromanundergroundreservoirisaccomplishedby theuseofnaturalreservoirenergy.27Thistypeofproductionistermedprimary production.Sources ofnaturalreservoirenergythatleadtoprimaryproductionincludetheswellingofreservoirfluids, thereleaseofsolutiongasasthereservoirpressuredeclines,nearbycommunicatingaquifers,gravitydrainage,andformationexpansion.Whenthereisnocommunicatingaquifer,thehydrocarbon recoveryisbroughtaboutmainlybytheswellingorexpansionofreservoirfluidsasthepressurein theformationdrops.However,inthecaseofoil,itmaybemateriallyaidedbygravitationaldrainage.Whenthereiswaterinfluxfromtheaquiferandthereservoirpressureremainsneartheinitial reservoirpressure,recoveryisaccomplishedbyadisplacementmechanism,whichagainmaybe aidedbygravitationaldrainage. 14 Chapter 1 • Introduction to Petroleum Reservoirs and Reservoir Engineering Whenthenaturalreservoirenergyhasbeendepleted,itbecomesnecessarytoaugmentthenaturalenergywithanexternalsource.Thisisusuallyaccomplishedbytheinjectionofgas(reinjected solutiongas,carbondioxide,ornitrogen)and/orwater.Theuseofaninjectionschemeiscalleda secondaryrecoveryoperation.Whenwaterinjectionisthesecondaryrecoveryprocess,theprocessis referredtoaswaterflooding.Themainpurposeofeitheranaturalgasorwaterinjectionprocessisto repressurizethereservoirandthenmaintainthereservoiratahighpressure.Hencethetermpressure maintenanceissometimesusedtodescribeasecondaryrecoveryprocess.Ofteninjectedfluidsalso displaceoiltowardproductionwells,thusprovidinganadditionalrecoverymechanism. Whengasisusedasthepressuremaintenanceagent,itisusuallyinjectedintoazoneoffree gas(i.e.,agascap)tomaximizerecoverybygravitydrainage.Theinjectedgasisusuallyproduced naturalgasfromthereservoirinquestion.This,ofcourse,defersthesaleofthatgasuntilthesecondaryoperationiscompletedandthegascanberecoveredbydepletion.Othergases,suchasnitrogen, canbeinjectedtomaintainreservoirpressure.Thisallowsthenaturalgastobesoldasitisproduced. Waterfloodingrecoversoilbythewatermovingthroughthereservoirasabankoffluidand “pushing”oilaheadofit.Therecoveryefficiencyofawaterfloodislargelyafunctionofthemacroscopicsweepefficiencyofthefloodandthemicroscopicporescaledisplacementbehaviorthat islargelygovernedbytheratiooftheoilandwaterviscosities.Theseconceptswillbediscussedin detailinChapters9,10,and11. Inmanyreservoirs,severalrecoverymechanismsmaybeoperatingsimultaneously,butgenerallyoneortwopredominate.Duringtheproducinglifeofareservoir,thepredominancemayshift fromonemechanismtoanothereithernaturallyorbecauseofoperationsplannedbyengineers.For example,initialproductioninavolumetricreservoirmayoccurthroughthemechanismoffluidexpansion.Whenitspressureislargelydepleted,thedominantmechanismmaychangetogravitational drainage,thefluidbeingliftedtothesurfacebypumps.Stilllater,watermaybeinjectedinsome wellstodriveadditionaloiltootherwells.Inthiscase,thecycleofthemechanismsisexpansion, gravitationaldrainage,displacement.Therearemanyalternativesinthesecycles,anditistheobject ofthereservoirengineertoplanthesecyclesformaximumrecovery,usuallyinminimumtime. Other displacement processes called tertiary recovery processes have been developed for applicationinsituationsinwhichsecondaryprocesseshavebecomeineffective.However,thesame processeshavealsobeenconsideredforreservoirapplicationswhensecondaryrecoverytechniques arenotusedbecauseoflowrecoverypotential.Inthislattercase,thewordtertiaryisamisnomer. Formostreservoirs,itisadvantageoustobeginasecondaryoratertiaryprocessbeforeprimary productioniscompleted.Forthesereservoirs,thetermenhanced oil recoverywasintroducedand hasbecomepopularinreferencetoanyrecoveryprocessthat,ingeneral,improvestherecovery overwhatthenaturalreservoirenergywouldbeexpectedtoyield.Enhancedoilrecoveryprocesses arepresentedindetailinChapter11. 1.6 Peak Oil Sinceoilisafiniteresourceinanygivenreservoir,itwouldmakesensethat,assoonasoilproductionfromthefirstwellbeginsinaparticularreservoir,theresourceofthatreservoirisdeclining. 1.6 Peak Oil 15 Asareservoirisdeveloped(i.e.,moreandmorewellsarebroughtintoproduction),thetotalproductionfromthereservoirwillincrease.Onceallthewellsthataregoingtobedrilledforagiven reservoirhavebeenbroughtintoproduction,thetotalproductionwillbegintodecline.M.King Hubberttookthisconceptanddevelopedthetermpeak oiltodescribenotthedeclineofoilproductionbutthepointatwhichareservoirreachesamaximumoilproductionrate.Hubbertsaidthis wouldoccuratthemidpointofreservoirdepletionorwhenone-halfoftheinitialhydrocarbonin placehadbeenproduced.28Hubbertdevelopedamathematicalmodelandfromthemodelpredicted thattheUnitedStateswouldreachpeakoilproductionsometimearoundtheyear1965.28AschematicofHubbert’spredictionisshowninFig.1.6. Figure1.7containsaplotoftheHubbertcurveandthecumulativeoilproductionfromall USreservoirs.ItwouldappearthatHubbertwasfairlyaccuratewithhismodelbutalittleoffon thetiming.However,theHubberttiminglooksmoreaccuratewhenproductionfromtheAlaskan NorthSlopeisomitted. Therearemanyfactorsthatgointobuildingsuchamodel.Thesefactorsincludeprovenreserves,oilprice,continuingexploration,continuingdemandonoilresources,andsoon.Manyof thesefactorscarrywiththemdebatesconcerningfuturepredictions.Asaresult,anargumentover theconceptofpeakoilhasdevelopedovertheyears.Itisnotthepurposeofthistexttodiscussthis argumentindetailbutsimplytopointoutsomeoftheprojectionsandsuggestthatthereadergoto theliteratureforfurtherinformation. 4 Peak production (or “midpoint depletion”) Production (bbl/year) 3 2 1 Cumulative production or ultimate recoverable resources (URR) 0 1800 Figure 1.6 1875 1900 1925 1950 Years 1975 The Hubbert curve for the continental United States. 2000 2025 2050 Chapter 1 16 • Introduction to Petroleum Reservoirs and Reservoir Engineering 11 10 9 Millions of barrels per day 8 7 6 5 4 3 2 1 0 1900 1910 1920 1930 1940 1950 US production Figure 1.7 1960 1970 1980 1990 2000 2010 Hubbert curve US crude oil production with the Hubbert curve (courtesy US Energy Information Administration). Hubbertpredictedthetotalworldcrudeoilproductionwouldreachthepeakaroundtheyear 2000.Figure1.8isaplotofthedailyworldcrudeoilproductionasafunctionofyear.Asonecan see,thepeakhasnotbeenreached—infact,theproductioniscontinuingtoincrease.Partofthe discrepancywithHubbert’spredictionhastodowiththeincreasingamountofworldreserves,as showninFig.1.9.Obviously,astheworld’sreservesincrease,thetimetoreachHubbert’speak willshift.Justasthereareseveralfactorsthataffectthetimeofpeakoil,thedefinitionofreserves hasseveralcontributingfactors,asdiscussedearlierinthischapter.Thispointwasillustratedina recentpredictionbytheInternationalEnergyAgency(IEA)regardingtheoilandgasproduction oftheUnitedStates.29 InarecentreportputoutbytheIEA,personnelpredictedthattheUnitedStateswillbecomethe world’stopoilproducerinafewyears.29Thisisinstarkcontrasttowhattheyhadbeenpredictingfor 1.6 Peak Oil 17 Million barrels per day 80 70 60 50 40 30 20 10 0 1975 Figure 1.8 1980 1985 1990 1995 Year 2000 2005 2010 2015 World crude oil production plotted as a function of year. 1600 Billion barrels 1400 1200 1000 800 600 400 200 0 1975 Figure 1.9 1980 1985 1990 1995 Year 2000 2005 2010 2015 World crude oil reserves plotted as a function of year. years.Thereportstatesthefollowing:“TherecentreboundinUSoilandgasproduction,drivenby upstreamtechnologiesthatareunlockinglighttightoilandshalegasresources,isspurringeconomic activity…andsteadilychangingtheroleofNorthAmericainglobalenergytrade.”29 Theupstreamtechnologiesthatarereferencedinthequotearetheincreaseduseofhydraulic fracturingandhorizontaldrillingtechniques.Thesetechnologiesarealargereasonfortheincrease inUSreservesfrom22.3billionbarrelsattheendof2009to25.2attheendof2010,whileproducingnearly2billionbarrelsin2010. Hydraulic fracturing or fracking referstotheprocessofinjectingahigh-pressurefluidintoa wellinordertofracturethereservoirformationtoreleaseoilandnaturalgas.Thismethodmakes 18 Chapter 1 • Introduction to Petroleum Reservoirs and Reservoir Engineering it possible to recover fuels from geologic formations that have poor flow rates. Fracking helps reinvigorate wells that otherwise would have been very costly to produce. Fracking has raised majorenvironmentalconcerns,andthereservoirengineershouldresearchthisprocessbeforerecommendingitsuse. Theuseofhorizontaldrillinghasbeeninexistencesincethe1920sbutonlyrelativelyrecently(1980s)reachedapointwhereitcouldbeusedonawidespreadscale.Horizontaldrilling isextremelyeffectiveforrecoveringoilandnaturalgasthatoccupyhorizontalstrata,becausethis methodoffersmorecontactareawiththeoilandgasthananormalverticalwell.Thereareendless possibilitiestotheusesofthismethodinhydrocarbonrecovery,makingitpossibletodrillinplaces thatareeitherliterallyimpossibleormuchtooexpensivetodowithtraditionalverticaldrilling. Theseincludehard-to-reachplaceslikedifficultmountainterrainoroffshoreareas. Hubbert’stheoryofpeakoilisreasonable;however,hispredictionshavenotbeenaccurate duetoincreasesinknownreservesandinthedevelopmentoftechnologiestoextractthepetroleum hydrocarbonseconomically.Reservoirengineeringistheformulationofaplantodevelopaparticularreservoirtobalancetheultimaterecoverywithproductioneconomics.Theremainderofthis textwillprovidetheengineerwithinformationtoassistinthedevelopmentofthatplan. Problems 1.1 Conductasearchonthewebandidentifytheworld’sresourcesandreservesofoilandgas. Whichcountriespossessthelargestamountofreserves? 1.2 Whataretheissuesinvolvedinacountry’sdefinitionofreserves?Writeashortreportthat discussestheissuesandhowacountrymightbeaffectedbytheissues. 1.3 Whataretheissuesbehindthepeakoilargument?Writeashortreportthatcontainsadescriptionofbothsidesoftheargument. 1.4 Theuseofhydraulicfracturinghasincreasedtheproductionofoilandgasfromtightsands, butitalsohasbecomeadebatabletopic.Whataretheissuesthatareinvolvedinthedebate? Writeashortreportthatcontainsadescriptionofbothsidesoftheargument. 1.5 Thecontinueddevelopmentofhorizontaldrillingtechniqueshasincreasedtheproductionof oilandgasfromcertainreservoirs.Conductasearchonthewebforapplicationsofhorizontaldrilling.Identifythreereservoirsinwhichthistechniquehasincreasedtheproductionof hydrocarbonsanddiscusstheincreaseinbothcostsandproduction. References 19 References 1. Principles of Petroleum Conservation, Engineering Committee, Interstate Oil Compact Commission,1955,2. 2. Society of Petroleum Engineers, “Petroleum Reserves and Resources Definitions,” http:// www.spe.org/industry/reserves.php 3. K.C.SclaterandB.R.Stephenson,“MeasurementsofOriginalPressure,Temperatureand Gas-OilRatioinOilSands,”Trans.AlME(1928–29),82,119. 4. C.V. Millikan and CarrolV. Sidwell, “Bottom-Hole Pressures in OilWells,” Trans.AlME (1931),92,194. 5. G.H.Fancher,J.A.Lewis,andK.B.Barnes,“SomePhysicalCharacteristicsofOilSands,” The Pennsylvania State College Bull.(1933),12,65. 6. R.D.Wyckoff,H.G.Botset,M.Muskat,andD.W.Reed,“MeasurementofPermeabilityof PorousMedia,”AAPG Bull.(1934),18,No.2,p.161. 7. R.D.WyckoffandH.G.Botset,“TheFlowofGas-LiquidMixturesthroughUnconsolidated Sands,”Physics(1936),7,325. 8. M.C.LeverettandW.B.Lewis,“SteadyFlowofOil-Gas-WaterMixturesthroughUnconsolidatedSands,”Trans.AlME(1941),142,107. 9. RalphJ.Schilthuis,“TechniqueofSecuringandExaminingSub-surfaceSamplesofOiland Gas,”Drilling and Production Practice,API(1935),120–26. 10. HowardC.PyleandP.H.Jones,“QuantitativeDeterminationoftheConnateWaterContentof OilSands,”Drilling and Production Practice,API(1936),171–80. 11. RalphJ.Schilthuis,“ConnateWaterinOilandGasSands,”Trans.AlME(1938),127,199–214. 12. C.V.Millikan,“TemperatureSurveysinOilWells,”Trans.AlME(1941),142,15. 13. RalphJ.Schilthuis,“ActiveOilandReservoirEnergy,”Trans.AlME(1936),118,33. 14. StewartColeman,H.D.WildeJr.,andThomasW.Moore,“QuantitativeEffectsofGas-Oil RatiosonDeclineofAverageRockPressure,”Trans.AlME(1930),86,174. 15. A.S.OdehandD.Havlena,“TheMaterialBalanceasanEquationofaStraightLine,”Jour. of Petroleum Technology(July1963),896–900. 16. W.Hurst,“WaterInfluxintoaReservoirandItsApplicationtotheEquationofVolumetric Balance,”Trans.AlME(1943),151,57. 17. A.F.vanEverdingenandW.Hurst,“ApplicationoftheLaPlaceTransformationtoFlowProblemsinReservoirs,”Trans.AlME(1949),186,305. 18. M.J.Fetkovich,“ASimplifiedApproachtoWaterInfluxCalculations—FiniteAquiferSystems,”Jour. of Petroleum Technology(July1971),814–28. 19. J.Tarner,“HowDifferentSizeGasCapsandPressureMaintenanceProgramsAffectAmount ofRecoverableOil,”Oil Weekly(June12,1944),144,No.2,32–44. 20 Chapter 1 • Introduction to Petroleum Reservoirs and Reservoir Engineering 20. S.E.BuckleyandM.C.Leverett,“MechanismofFluidDisplacementinSands,”Trans.AlME (1942),146,107–17. 21. M.Muskat,“ThePetroleumHistoriesofOilProducingGas-DriveReservoirs,”Jour. of Applied Physics(1945),16,147. 22. A.Odeh,“ReservoirSimulation—WhatIsIt?,”Jour. of Petroleum Technology(Nov.1969), 1383–88. 23. K.H.Coats,“UseandMisuseofReservoirSimulationModels,”Jour. of Petroleum Technology(Nov.1969),1391–98. 24. K.H.Coats,“ReservoirSimulation:StateoftheArt,”Jour. of Petroleum Technology(Aug. 1982),1633–42. 25. T.V.Moore,“ReservoirEngineeringBeginsSecond25Years,”Oil and Gas Jour.(1955),54, No.29,148. 26. NormanJ.ClarkandArthurJ.Wessely,“CoordinationofGeologyandReservoirEngineering— AGrowingNeedforManagementDecisions,”presentedbeforeAPI,DivisionofProduction,Mar. 1957. 27. R.E.Terry,“EnhancedOilRecovery,”Encyclopedia of Physical Science and Technology, Vol. 5,3rded.,AcademicPress,2002. 28. M.K.Hubbert,“NuclearEnergyandtheFossilFuels,”Proc.AmericanPetroleumInstitute DrillingandProductionPractice,SpringMeeting,SanAntonio(1956),7–25;seealsoShell DevelopmentCompanyPublication95,June1956. 29. InternationalEnergyAgency,“WorldEnergyOutlook2012ExecutiveSummary,”http://www .iea.org/publications/freepublications/publication/English.pdf C H A P T E R 2 Review of Rock and Fluid Properties 2.1 Introduction Asfluidfromareservoirisproducedandbroughttothesurface,thefluidremaininginthereservoirexperienceschangesinthereservoirconditions.Theproducedfluidalsoexperienceschangesasitisbroughttothesurface.Thereservoirfluidtypicallyseesonlyadecreaseinpressure, whiletheproducedfluidwillexperiencedecreasesinpressureandintemperature.Asthepressure decreases,itiscommontoobservegasthathadbeendissolvedintheoilorwaterbeliberated. Reservoirengineersuseterms,suchasthesolutiongas-oilratio(Rso),toaccountforthis.There aremanyvariationsonthisterm.Risgenerallyusedtodenoteanyratio,whilethesubscriptsdenotewhichratioisbeingused.Rsoi,forexample,istheinitialgas-oilratio,andRswisthesolution gas-waterratio. Asthefluidisproducedfromthereservoir,thepressureontherockfromtheoverburdenor therockaboveitremainsconstantbutthepressureofthefluidsurroundingitisdecreasing.This leadstherocktoexpandortheporesintherocktobecompressed.Thischangeinporevolume duetopressureiscalledthepore volume compressibility(cf).Thecompressibilityofthegasisalso ofinterest.Thegascompressibility(cg)involvesacompressibilityfactor(z).Thecompressibility factorissimplyaratioofhowthegaswouldbehaveideallycomparedtohowitbehavesinactuality.Thecompressibilityofoil(co)andwater(cw)canalsobedetermined,buttheirmagnitudeisfar lessthanthatofthegas.Thedeterminationofeachoftheseproperties,aswellasthosedefinedin Chapter1,iscriticalinpredictingtheperformanceofareservoir.Thischaptercontainsadiscussion ofthepertinentrockandfluidpropertieswithwhichareservoirengineerwillwork. 2.2 Review of Rock Properties Propertiesdiscussedinthissectionincludeporosity,isothermalcompressibility,andfluidsaturation.Althoughpermeabilityisapropertyofarockmatrix,becauseofitsimportanceinfluidflow calculations,adiscussionofpermeabilityispostponeduntilChapter8,inwhichsingle-phasefluid flowisconsidered. 21 Chapter 2 22 2.2.1 • Review of Rock and Fluid Properties Porosity AsdiscussedinChapter1,theporosityofaporousmediumisgiventhesymbolof φ and is definedastheratioofvoidspace,orporevolume,tothetotalbulkvolumeoftherock.Thisratiois expressedaseitherafractionorapercentage.Whenusingavalueofporosityinanequation,it isnearlyalwaysexpressedasafraction.Thetermhydrocarbon porosityreferstothatpartofthe porositythatcontainshydrocarbon.Itisthetotalporositymultipliedbythefractionofthepore volume that contains hydrocarbon. Porosity values range from 10% to 40% for sandstone type reservoirsand5%to15%forlimestonetypereservoirs.1 Thevalueofporosityisusuallyreportedaseitheratotaloraneffectiveporosity,dependingonthetypeofmeasurementused.Thetotalporosityrepresentsthetotalvoidspaceofthe medium.Theeffectiveporosityistheamountofthevoidspacethatcontributestotheflowof fluids.Thisisthetypeofporosityusuallymeasuredinthelaboratoryandusedincalculations offluidflow. The laboratory methods of measuring porosity include Boyle’s law, water saturation, and organic-liquidsaturationmethods.Dotson,Slobod,McCreery,andSpurlockhavedescribedaporosity-checkprogrammadeby5laboratorieson10samples.2Theaveragedeviationofporosity fromtheaveragevalueswas±0.5%porosity.Theaccuracyoftheaverageporosityofareservoir asfoundfromcoreanalysisdependsonthequalityandquantityofthedataavailableandonthe uniformity of the reservoir. The average porosity is seldom known more precisely than to 1% porosity(e.g.,to5%accuracyat20%porosity).Theporosityisalsocalculatedfromindirectmethodsusingwelllogdata,oftenwiththeassistanceofsomecoremeasurements.Ezekwediscusses theuseofvarioustypesofwelllogsinthecalculationofporosity.3Loggingtechniqueshavethe advantageofaveraginglargervolumesofrockthanincoreanalysis.Whencalibratedwithcore data,theyshouldprovideaverageporosityfiguresinthesamerangeofaccuracyascoreanalysis. Whentherearevariationsinporosityacrossthereservoir,theaverageporosityshouldbefoundon avolume-weightedbasis.Inhighlyfractured,rubblized,orvuggycarbonatereservoirs,thehighest porosityrockmaybeneithercorednorlogged,andhydrocarbonvolumesbasedoncoreorlog porosityaveragesmaybegrosslyunderestimated. 2.2.2 Isothermal Compressibility Theisothermalcompressibilityforasubstanceisgivenbythefollowingequation: c=− where c=isothermalcompressibility V=volume p=pressure 1 dV V dp (2.1) 2.2 Review of Rock Properties 23 Theequationdescribesthechangeinvolumethatasubstanceundergoesduringachangeinpressurewhilethetemperatureisheldconstant.Theunitsareinreciprocalpressureunits.Whenthe internalfluidpressurewithintheporespacesofarock,whichissubjectedtoaconstantexternal (rockoroverburden)pressure,isreduced,thebulkvolumeoftherockdecreaseswhilethevolume ofthesolidrockmaterial(e.g.,thesandgrainsofasandstone)increases.Bothvolumechangesact toreducetheporosityoftherockslightly,oftheorderof0.5%fora1000-psichangeintheinternal fluidpressure(e.g.,at20%porosityto19.9%). Studies by van der Knaap indicate that this change in porosity for a given rock depends onlyonthedifferencebetweentheinternalandexternalpressuresandnotontheabsolutevalue of the pressures.4As with the volume of reservoir coils above the bubble point, however, the changeinporevolumeisnonlinearandtheporevolumecompressibilityisnotconstant.Thepore volume compressibility (cf)atanyvalueofexternal-internalpressuredifferencemaybedefined asthechangeinporevolumeperunitofporevolumeperunitchangeinpressure.Thevaluesfor limestoneandsandstonereservoirrockslieintherangeof2×10–6to25×10–6 psi–1.Ifthecompressibilityisgivenintermsofthechangeinporevolumeperunitofbulkvolumeperunitchange inpressure,dividingbythefractionalporosityplacesitonaporevolumebasis.Forexample,a compressibilityof1.0×10–6porevolumeperbulkvolumeperpsiforarockof20%porosityis 5.0×10–6porevolumeperporevolumeperpsi. Newmanmeasuredisothermalcompressibilityandporosityvaluesin79samplesofconsolidatedsandstonesunderhydrostaticpressure.5Whenhefitthedatatoahyperbolicequation,he obtainedthefollowingcorrelation: cf = 97.3200(10 )−6 (1 + 55.8721φ )1.42859 (2.2) Thiscorrelationwasdevelopedforconsolidatedsandstoneshavingarangeofporosityvaluesfrom 0.02< φ<0.23.Theaverageabsoluteerrorofthecorrelationovertheentirerangeofporosity valueswasfoundtobe2.60%. Newmanalsodevelopedasimilarcorrelationforlimestoneformationsunderhydrostatic pressure.5Therangeofporosityvaluesincludedinthecorrelationwas0.02<φ<0.33,andthe averageabsoluteerrorwasfoundtobe11.8%.Thecorrelationforlimestoneformationsisas follows: cf = 0.853531 (1 + 2.47664 (10 )6φ )0.92990 (2.3) Eventhoughtherockcompressibilitiesaresmallfigures,theireffectmaybeimportantin somecalculationsonreservoirsoraquifersthatcontainfluidsofcompressibilitiesintherangeof 3to25(10)–6 psi–1.OneapplicationisgiveninChapter6involvingcalculationsabovethebubble point.Geertsmapointsoutthatwhenthereservoirisnotsubjectedtouniformexternalpressure,as Chapter 2 24 • Review of Rock and Fluid Properties arethesamplesinthelaboratorytestsofNewman,theeffectivevalueinthereservoirwillbeless thanthemeasuredvalue.6 2.2.3 Fluid Saturations Theratioofthevolumethatafluidoccupiestotheporevolumeiscalledthesaturationofthatfluid. ThesymbolforoilsaturationisSo,whereSreferstosaturationandthesubscriptoreferstooil. Saturationisexpressedaseitherafractionorapercentage,butitisusedasafractioninequations. Thesaturationsofallfluidspresentinaporousmediumaddto1. Thereare,ingeneral,twowaysofmeasuringoriginalfluidsaturations:thedirectapproach andtheindirectapproach.Thedirectapproachinvolveseithertheextractionofthereservoirfluids ortheleachingofthefluidsfromasampleofthereservoirrock.Theindirectapproachreliesona measurementofsomeotherproperty,suchascapillarypressure,andthederivationofamathematicalrelationshipbetweenthemeasuredpropertyandsaturation. Directmethodsincluderetortingthefluidsfromtherock,distillingthefluidswithamodified AmericanSocietyforTestingandMaterials(ASTM)procedure,andcentrifugingthefluids.Each methodreliesonsomeproceduretoremovetherocksamplefromthereservoir.Experiencehas foundthatitisdifficulttoremovethesamplewithoutalteringthestateofthefluidsand/orrock. Theindirectmethodsuseloggingorcapillarypressuremeasurements.Witheithermethod,errors are built into the measurement of saturation. However, under favorable circumstances and with carefulattentiontodetail,saturationvaluescanbeobtainedwithinusefullimitsofaccuracy.Ezekwepresentsmodelsandequationsusedinthecalculationofsaturationvaluesforbothdirectand indirectmethods.3 2.3 2.3.1 Review of Gas Properties Ideal Gas Law Relationshipsthatdescribethepressure-volume-temperature(PVT)behaviorofgasesarecalled equations of state.Thesimplestequationofstateiscalledtheideal gas lawandisgivenby pV = nR′T (2.4) where p=absolutepressure V=totalvolumethatthegasoccupies n=molesofgas T=absolutetemperature R′=gasconstant WhenR′=10.73,pmustbeinpoundspersquareinchabsolute(psia),Vincubicfeet(ft3),n in pound-moles (lb-mols), and T in degrees Rankine (°R).The ideal gas law was developed from Boyle’sandCharles’slaws,whichwereformedfromexperimentalobservations. 2.3 Review of Gas Properties 25 Thepetroleumindustryworkswithasetofstandardconditions—usually14.7psiaand60°F. Whenavolumeofgasisreportedattheseconditions,itisgiventheunitsofSCF(standardcubic feet).AsmentionedinChapter1,sometimestheletterMwillappearintheunits(e.g.,MCFor MSCF).Thisrefersto1000standardcubicfeet.Thevolumethat1lb-moloccupiesatstandard conditionsis379.4SCF.Aquantityofapuregascanbeexpressedasthenumberofcubicfeetata specifiedtemperatureandpressure,thenumberofmoles,thenumberofpounds,orthenumberof molecules.Forpracticalmeasurement,theweighingofgasesisdifficult,sogasesaremeteredby volumeatmeasuredtemperaturesandpressures,fromwhichthepoundsormolesmaybecalculated.Example2.1illustratesthecalculationsofthecontentsofatankofgasineachofthreeunits. Example 2.1 Calculating the Contents of a Tank of Ethane in Moles, Pounds, and SCF Given A500-ft3tankofethaneat100psiaand100°F. Solution Assumingidealgasbehavior, Moles = 100 × 500 = 8.32 10.73 × 560 Pounds=8.32×30.07=250.2 At14.7psiaand60°F, SCF=8.32×379.4=3157 HereisanalternatesolutionusingEq.(2.4): SCF = 2.3.2 nR ' T 8.32 × 10.73 × 520 = = 3158 p 14.7 Specific Gravity Becausethedensityofasubstanceisdefinedasmassperunitvolume,thedensityofgas,ρg,ata giventemperatureandpressurecanbederivedasfollows: pV Mw pM w density = ρg = R ' T = V R 'T density = nM w mass = V volume (2.5) Chapter 2 26 • Review of Rock and Fluid Properties where Mw = molecular weight Becauseitismoreconvenienttomeasurethespecificgravityofgasesthanthegasdensity,specific gravityismorecommonlyused.Specific gravityisdefinedastheratioofthedensityofagasata giventemperatureandpressuretothedensityofairatthesametemperatureandpressure,usually near 60°F and atmospheric pressure.Whereas the density of gases varies with temperature and pressure,thespecificgravityisindependentoftemperatureandpressurewhenthegasobeysthe idealgaslaw.Bythepreviousequation,thedensityofairis ρair = p × 28.97 R 'T Thenthespecificgravity,γg,ofagasis pM w ρg Mw R'T γg = = = p × 28.97 28.97 ρair R 'T (2.6) Equation(2.6)mightalsohavebeenobtainedfromthepreviousstatementthat379.4ft3of anyidealgasat14.7psiaand60°Fis1molandthereforeaweightequaltothemolecularweight. Thus,bydefinitionofspecificgravity, γg = Mw Weightof379.4ft 3 of gas at14.7and60°F = Weeightof379.4ft 3 of air at14.7and60°F 28.97 Ifthespecificgravityofagasis0.75,itsmolecularweightis21.7lbspermol. 2.3.3 Real Gas Law Everythinguptothispointappliestoaperfectoridealgas.Actuallytherearenoperfectgases; however,manygasesnearatmospherictemperatureandpressureapproachidealbehavior.All moleculesofrealgaseshavetwotendencies:(1)toflyapartfromeachotherbecauseoftheir constantkineticmotionand(2)tocometogetherbecauseofelectricalattractiveforcesbetween themolecules.Becausethemoleculesarequitefarapart,theintermolecularforcesarenegligibleandthegasbehavesclosetoideal.Also,athightemperatures,thekineticmotion,being greater, makes the attractive forces comparatively negligible and, again, the gas approaches idealbehavior. Whenthevolumeofagaswillbelessthanwhattheidealgasvolumewouldbe,thegasissaid tobesupercompressible.Thenumber,whichmeasuresthegas’sdeviationfromperfectbehavior, 2.3 Review of Gas Properties 27 issometimescalledthesupercompressibility factor,usuallyshortenedtothegas compressibility factor.Morecommonlyitiscalledthegas deviation factor(z).Thisdimensionlessquantityusually variesbetween0.70and1.20,withavalueof1.00representingidealbehavior. Atveryhighpressures,aboveabout5000psia,naturalgasespassfromasupercompressible conditiontooneinwhichcompressionismoredifficultthanintheidealgas.Theexplanationis that,inadditiontotheforcesmentionedearlier,whenthegasishighlycompressed,thevolume occupiedbythemoleculesthemselvesbecomesanappreciableportionofthetotalvolume.Sinceit isreallythespacebetweenthemoleculesthatiscompressedandthereislesscompressiblespace, thegasappearstobemoredifficulttocompress.Inaddition,asthemoleculesgetclosertogether (i.e.,athighpressure),repulsiveforcesbegintodevelopbetweenthemolecules.Thisisindicated byagasdeviationfactorgreaterthanunity.Thegasdeviationfactorisbydefinitiontheratioof thevolumeactuallyoccupiedbyagasatagivenpressureandtemperaturetothevolumeitwould occupyifitbehavedideally,or z= Va Actual volume of n moles of gas at T and p = Vi Ideal volume of n moles at same T and p (2.7) Thesetheoriesqualitativelyexplainthebehaviorofnonidealorrealgases.Equation(2.7) maybesubstitutedintheidealgaslaw,Eq.(2.4),togiveanequationforusewithnonidealgases, V p a = nR ' T or pVa = znR ' T z (2.8) whereVaistheactualgasvolume.Thegasdeviationfactormustbedeterminedforeverygasand everycombinationofgasesandatthedesiredtemperatureandpressure—foritisdifferentforeach gasormixtureofgasesandforeachtemperatureandpressureofthatgasormixtureofgases.The omissionofthegasdeviationfactoringasreservoircalculationsmayintroduceerrorsaslargeas 30%.7Figure2.1showsthegasdeviationfactorsoftwogases,oneof0.90specificgravityandthe otherof0.665specificgravity.Thesecurvesshowthatthegasdeviationfactorsdropfromunity atlowpressurestoaminimumvaluenear2500psia.Theyriseagaintounitynear5000psiaand tovaluesgreaterthanunityatstillhigherpressures.Intherangeof0to5000psia,thedeviation factorsatthesametemperaturewillbelowerfortheheaviergas,andforthesamegas,theywillbe loweratthelowertemperature. Whenpossiblereservoirfluidsamplesshouldbeacquiredattheformationlevel,suchsamples are termed bottom-hole fluid samples, and great care must be taken to avoid sampling the reservoir fluid below bubble-point or dew-point pressure. Without a bottom-hole fluid sample, producedwetgasorgascondensatemayberecombinedatthesurface.Thismaybeaccomplished byrecombiningsamplesofseparatorgas,stock-tankgas,andstock-tankliquidintheproportions inwhichtheyareproduced.Thedeviationfactorismeasuredatreservoirtemperatureforpressures rangingfromreservoirtoatmospheric.Forwetgasorgascondensate,thedeviationfactormay bemeasuredfordifferentiallyliberatedgasbelowthedew-pointpressure.Forreservoiroil,the Chapter 2 28 • Review of Rock and Fluid Properties Compressibility factor, z 1.20 1.10 Temp. 250ºF Gravity 0.665 1.00 Temp. 150ºF Gravity 0.665 .90 .80 Temp. 150ºF Gravity 0.90 .70 .60 0 1000 2000 3000 4000 5000 6000 Reservoir pressure in psi Figure 2.1 Effect of pressure, temperature, and composition on the gas deviation factor. deviationfactorofsolutiongasismeasuredongassamplesevolvedfromsolutionintheoilduring adifferentialliberationprocess. The gas deviation factor is commonly determined by measuring the volume of a sample at desiredpressuresandtemperaturesandthenmeasuringthevolumeofthesamemassofgasatatmosphericpressureandatatemperaturesufficientlyhighsothatallthematerialremainsinthevapor phase.Forexample,asampleoftheBellFieldgashasameasuredvolumeof364.6cm3at213°Fand 3250psia.At14.80psiaand82°F,ithasavolumeof70,860cm3.Then,byEq.(2.8),assumingagas deviationfactorofunityatthelowerpressure,thedeviationfactorat3250psiaand213°Fis z= 3250 × 364.6 1.00 × ( 460 + 82 ) × = 0..910 460 + 213 14.80 × 70, 860 If the gas deviation factor is not measured, it may be estimated from its specific gravity. Example2.2showsthemethodforestimatingthegasdeviationfactorfromitsspecificgravity. Themethodusesacorrelationtoestimatepseudocriticaltemperatureandpressurevaluesforagas withagivenspecificgravity.ThecorrelationwasdevelopedbySuttononthebasisofover5000 differentgassamples.8Suttondevelopedacorrelationfortwodistincttypesofgases—onebeingan associatedgasandtheotherbeingacondensategas.Anassociatedgasisdefinedasagasthathas beenliberatedfromoilandtypicallycontainslargeconcentrationsofethanethroughpentane.A condensategastypicallycontainsavaporizedhydrocarbonliquid,resultinginahighconcentration oftheheptanes-plusfractionsinthegasphase. 2.3 Review of Gas Properties 29 Fortheassociatedgases,Suttonconductedaregressionanalysisontherawdataandobtained thefollowingequationsovertherangeofspecificgasgravitieswithwhichheworked—0.554<γg <1.862: ppc=671.1+14.0γg–34.3γg2 (2.9) Tpc=120.1+429γg–62.9γg2 (2.10) Suttonfoundthefollowingequationsforthecondensategasescoveringtherangeofgasgravities of0.554<γg<2.819: ppc=744–125.4γg+5.9γg2 (2.11) Tpc=164.3+357.7γg–67.7γg2 (2.12) Bothsetsofthesecorrelationswerederivedforgasescontaininglessthan10%ofH2S, CO2, and N2.Ifconcentrationsofthesegasesarelargerthan10%,thereaderisreferredtotheoriginalwork ofSuttonforcorrections. Havingobtainedthepseudocriticalvalues,thepseudoreducedpressureandtemperatureare calculated.ThegasdeviationfactoristhenfoundbyusingthecorrelationchartofFig.2.2. Example 2.2 Calculating the Gas Deviation Factor of a Gas Condensate from Its Specific Gravity Given Gasspecificgravity=0.665 Reservoirtemperature=213°F Reservoirpressure=3250psia Solution UsingEqs.(2.11)and(2.12),thepseudocriticalvaluesare ppc=744–125.4(0.665)+5.9(0.665)2=663psia Tpc=164.3+357.7(0.665)–67.7(0.665)2=372°R For3250psiaand213°F,thepseudoreducedpressureandtemperatureare p pr = 3250 = 4.90 663 Pseudoreduced pressure 0 1 2 3 1.1 4 5 6 7 1.1 Pseudoreduced temperature 3.0 2.8 2.6 2.4 2.2 2.0 1.9 1.8 1.0 0.9 8 1.0 1.3 1.1 1.05 1.2 0.9 1.7 5 1.0 1 . 1 1.6 0.8 1.5 1.7 Compressibility factor, z 1.45 1.2 1.4 0.7 1.35 1.6 1.3 1.3 0.6 1.4 1.5 1.6 1.7 1.25 1.2 1.8 1.9 2.0 2.2 0.5 1.15 0.4 1.5 1.3 2.4 2.6 3.0 1.1 1.4 1.2 0.3 1.05 3.0 2.8 1.1 2.6 2.2 2.0 1.8 1.7 1.6 1.0 0.9 7 1.1 2.4 1.9 1.2 1.1 1.05 1.0 1.4 1.3 8 0.9 9 10 11 12 13 14 15 Pseudoreduced pressure Figure 2.2 Compressibility factors for natural gases (after Standing and Katz, trans. AlME).9 30 2.3 Review of Gas Properties 31 T pr = 460 + 213 = 1.81 372 UsingthecalculatedvaluesinFig.2.2,z=0.918. Inmanyreservoir-engineeringcalculations,itisnecessarytousetheassistanceofacomputer, andthechartofStandingandKatzthenbecomesdifficulttouse.DranchukandAbou-Kassemfitan equationofstatetothedataofStandingandKatzinordertoestimatethegasdeviationfactorincomputerroutines.10DranchukandAbou-Kassemused1500datapointsandfoundanaverageabsolute errorof0.486%overrangesofpseudoreducedpressureandtemperatureof 0.2<ppr<30 andfor 1.0<Tpr<3.0 ppr<1.0with0.7<Tpr<1.0 TheDranchukandAbou-KassemequationofstategivespoorresultsforTpr=1.0andppr>1.0.The formoftheDranchukandAbou-Kassemequationofstateisasfollows: where z=1+c1(Tpr)ρr + c2(Tpr) ρr2 – c3(Tpr)ρr5 + c4(ρr, Tpr) (2.13) ρr=0.27ppr/(z Tpr) (2.13a) c1(Tpr)=0.3265–1.0700/Tpr –0.5339/Tpr3 + 0.01569/Tpr4 –0.05165/ T pr5 (2.13b) c2(Tpr)=0.5475–0.7361/Tpr + 0.1844/T pr2 (2.13c) c3(Tpr)=0.1056(–0.7361/Tpr + 0.1844/T pr2 ) (2.13d) c4(ρr, Tpr)=0.6134(1+0.7210ρr2)(ρ2r/T pr3 )exp(–0.7210ρr2) (2.13e) Becausethez-factorisonbothsidesoftheequation,aniterativemethodisnecessarytosolve theDranchukandAbou-Kassemequationofstate.Anyoneofanumberoftechniquescanbeused toassistintheiterativemethod.11TheExcelsolverfunctionisacommoncomputertooltosolve thesetypesofiterativeproblems,andinstructionsonitsuseareavailableintheHelpsectionofthe Excelprogram. Table 2.1 Physical Properties of the Paraffin Hydrocarbons and Other Compounds (after Eilerts12) Critical constants Molecular weight Boiling point at 14.7 psia °F Methane 16.04 Ethane Compound 32 a Pressure, pe, psia Temperature Te, °R –258.7 673.1 343.2 a 30.07 –127.5 708.3 549.9 a Propane 44.09 –43.7 617.4 666.0 b Isobutane 58.12 10.9 529.1 734.6 b n-Butane 58.12 31.1 550.1 765.7 b Isopentane 72.15 82.1 483.5 n-Pentane 72.15 96.9 489.8 Est. part. volume at 60°F, 14.7 psia, gal per M SCF Est. part. volume at 60° F, 14.4 psia, gal per lb-mole G (grams) per cc lb per gal 0.348 2.90 14.6 5.53 0.485 4.04 19.6 7.44 0.5077 4.233 27.46 10.417 0.5631 4.695 32.64 12.380 0.5844 4.872 31.44 11.929 829.6 0.6248 5.209 36.50 13.851 846.2 0.6312 5.262 36.14 13.710 n-Hexane 86.17 155.7 440.1 914.2 0.6641 5.536 41.03 15.565 n-Heptane 100.2 209.2 395.9 972.4 0.6882 5.738 46.03 17.463 n-Octane 114.2 258.2 362.2 1024.9 0.7068 5.892 51.09 19.385 n-Nonane 128.3 303.4 334 1073 0.7217 6.017 56.19 21.314 n-Decane 142.3 345.4 312 1115 0.7341 6.121 61.27 23.245 Air 28.97 –317.7 547 239 Carbon dioxide 44.01 –109.3 1070.2 547.5 Helium 4.003 –452.1 33.2 9.5 Hydrogen 2.106 –423.0 189.0 59.8 Hydrogen sulfide 34.08 –76.6 1306.5 672.4 0.9990 8.337 Nitrogen 28.02 –320.4 492.2 227.0 Oxygen 32.00 –297.4 736.9 278.6 Water 18.0 2212.0 3209.5 1165.2 Basispartialvolumeinsolution. Atbubble-pointpressureand60°F. b Liquid density 60°F, 14.7 psia 2.3 Review of Gas Properties 33 Amoreaccurateestimationofthedeviationfactorcanbemadewhentheanalysisofthe gasisavailable.Thiscalculationassumesthateachcomponentcontributestothepseudocritical pressureandtemperatureinproportiontoitsvolumepercentageintheanalysisandtothecritical pressureandtemperature,respectively,ofthatcomponent.Table2.1givesthecriticalpressures andtemperaturesofthehydrocarboncompoundsandotherscommonlyfoundinnaturalgases.12 Italsogivessomeadditionalphysicalpropertiesofthesecompounds.Example2.3showsthe methodofcalculatingthegasdeviationfactorfromthecompositionofthegas. Example 2.3 Calculating the Gas Deviation Factor of the Bell Field Gas from Its Composition Given Thecompositioncolumn2andthephysicaldatacolumns3to5aretakenfromTable2.1. (1) Component (2) Component, mole fraction (3) Molecular weight (4) pc (5) Tc (6) (2) × (3) Methane 0.8612 16.04 673 343 Ethane 0.0591 30.07 708 550 Propane 0.0358 44.09 617 Butane 0.0172 58.12 550 (7) (2) × (4) (8) (2) × (5) 13.81 579.59 295.39 1.78 41.84 32.51 666 1.58 22.09 23.84 766 1.00 9.46 13.18 Pentanes 0.0050 72.15 490 846 0.36 2.45 4.23 CO2 0.0010 44.01 1070 548 0.04 1.07 0.55 N2 0.0207 28.02 492 227 0.58 10.18 4.70 Total 1.0000 19.15 666.68 374.40 Solution Thespecificgravitymaybeobtainedfromthesumofcolumn6,whichistheaveragemolecular weightofthegas, γg = 19.15 = 0.661 28.97 Thesumsofcolumns7and8arethepseudocriticalpressureandtemperature,respectively.Then, at3250psiaand213°F,thepseudoreducedpressureandtemperatureare Chapter 2 34 • p pr = 3250 = 4.87 666.68 T pr = 673 = 1.80 374.3 Review of Rock and Fluid Properties ThegasdeviationfactorusingFig.2.2isz=0.91. WichertandAzizhavedevelopedacorrelationtoaccountforinaccuraciesintheStanding andKatzchartwhenthegascontainssignificantfractionsofcarbondioxide(CO2)andhydrogen sulfide(H2S).13TheWichertandAzizcorrelationmodifiesthevaluesofthepseudocriticalconstantsofthenaturalgas.Oncethemodifiedconstantsareobtained,theyareusedtocalculatepseudoreducedproperties,asdescribedinExample2.2,andthez-factorisdeterminedfromFig.2.2or Eq.(2.13).TheWichertandAzizcorrelationequationisasfollows: ε=120(A0.9 – A1.6)+15(B0.5 – B4) (2.14) where A=sumofthemolefractionsofCO2andH2Sinthegasmixture B=molefractionofH2Sinthegasmixture Themodifiedpseudocriticalpropertiesaregivenby T pc' = T pc − ε p 'pc = p pcT pc' (T pc + B(1 − B)ε ) (2.14a) (2.14b) WichertandAzizfoundtheircorrelationtohaveanaverageabsoluteerrorof0.97%overthefollowingrangesofdata:154<p(psia)<7026and40<T(°F)<300.Thecorrelationisgoodfor concentrationsofCO2<54.4%(mol%)andH2S<73.8%(mol%). 2.3.4 Formation Volume Factor and Density The gas formation volume factor(Bg)relatesthevolumeofgasinthereservoirtothevolumeon thesurface(i.e.,atstandardconditionspsc and Tsc).Itisgenerallyexpressedineithercubicfeetor barrelsofreservoirvolumeperstandardcubicfootofgas.Assumingagasdeviationfactorofunity forthestandardconditions,thereservoirvolumeof1stdft3atreservoirpressurepandtemperature TbyEq.(2.8)is 2.3 Review of Gas Properties 35 Bg = psc zT Tsc p (2.15) wherepscis14.7psiaandTscis60°F: Bg = 0.02829 zT 3 zT ft /SCFBg = 0.00504 bbl/SCF p p (2.16) TheconstantsinEq.(2.16)arefor14.7psiaand60°Fonly,anddifferentconstantsmustbecalculatedforotherstandards.ThusfortheBellFieldgasatareservoirpressureof3250psia,atemperatureof213°F,andagasdeviationfactorof0.910,thegasvolumefactoris Bg = 0.02829 × 0.910 × 673 = 0.0053 ft 3 /SCF 3250 Thesegasvolumefactorsmeanthat1stdft3(at14.7psiaand60°F)willoccupy0.00533ft3of spaceinthereservoirat3250psiaand213°F.Becauseoilisusuallyexpressedinbarrelsandgas incubicfeet,whencalculationsaremadeoncombinationreservoirscontainingbothgasandoil, eithertheoilvolumemustbeexpressedincubicfeetorthegasvolumeinbarrels.Theforegoing gasvolumefactorexpressedinbarrelsis0.000949bbl/SCF.Then1000ft3ofreservoirporevolume intheBellFieldgasreservoirat3250psiacontains G=1000ft3÷0.00533ft3/SCF=188MSCF Equation(2.8)mayalsobeusedtocalculatethedensityofareservoirgas.Anexpressionfor themolesofgasin1ft3ofreservoirgasporespaceisp/zRT.ByEq.(2.6),themolecularweightof agasis28.97× γglbpermol.Therefore,thepoundscontainedin1ft3—thatis,thereservoir gas density(ρg)—is ρg = 28.97 × γ g × p zR ' T Forexample,thedensityoftheBellFieldreservoirgaswithagasgravityof0.665is ρg = 2.3.5 28.97 × 0.665 × 3250 = 9.530 lb/cufft 0.910 × 10.73 × 673 Isothermal Compressibility Thechangeinvolumewithpressureforgasesunderisothermalconditions,whichiscloselyrealizedinreservoirgasflow,isexpressedbytherealgaslaw: Chapter 2 36 V= • Review of Rock and Fluid Properties znR ' T z orV = constant × p p (2.17) Sometimesitisusefultointroducetheconceptofgas compressibility.Thismustnotbeconfused withthegasdeviationfactor,whichisalsoreferredtoasthegascompressibility factor.Equation (2.17)maybedifferentiatedwithrespecttopressureatconstanttemperaturetogive dv nR ' T dz znR ' T = − dp p dp p2 znR ' T 1 dz znR ' t 1 × = − p z dp p p 1 dV 1 dz 1 × = − V dp z dp p Finally,because c=− cg = 1 dV V dp 1 1 dz − p z dp (2.18) foranidealgas,z=1.00anddz/dp = 0,andthecompressibilityissimplythereciprocalofthepressure.Anidealgasat1000psia,then,hasacompressibilityof1/1000or1000×10–6 psi–1.Example 2.4showsthecalculationofthecompressibilityofagasfromthegasdeviationfactorcurveof Fig.2.4usingEq.(2.18). Example 2.4 Finding the Compressibility of a Gas from the Gas Deviation Factor Curve Given Thegasdeviationfactorcurveforagasat150°FisshowninFig.2.3. Solution At1000psia,theslopedz/dpisshowngraphicallyinFig.2.3as–127×10–6.Notethatthisisa negativeslope.Then,becausez=0.83 1 1 − ( −127 × 10 −6 ) 1000 0.83 = 1000 × 10 −6 + 153 × 10 −6 = 1153 × 10 −6 psi−1 cg = 2.3 Review of Gas Properties 37 At2500psia,theslopedz/dpiszero,sothecompressibilityissimply cg = 1 = 400 × 10 −6 psi−1 2500 At4500psia,theslopedz/dpispositiveand,asshowninFig.2.3,isequalto110×10–6psi–1. Sincez=0.90at4500psia, cg = 1 1 − (110 × 10 −6 ) 4500 0.90 =222×10–6–122×10–6=100×10–6psi–1 1.1 Slope at 1000 psia ∆Z = –0.19 = –127 × 10–6 psi–1 ∆P 1500 ∆Z = 0.22 0.9 ∆Z = 0.19 Gas deviation factor, z 1.0 Slope at 4500 psia ∆Z = 0.22 = 110 × 10–6 psi–1 2000 ∆P 0.8 ∆P = 2000 ∆P = 1500 0.7 0.6 Slope at 2500 psia is zero. 0 1000 2000 3000 Pressure, psia 4000 5000 6000 Figure 2.3 Gas compressibility from the gas deviation factor versus pressure plot (see Example 2.4). Chapter 2 38 • Review of Rock and Fluid Properties TrubehasreplacedthepressureinEq.(2.18)bytheproductofthepseudocriticalandthe pseudoreducedpressures,orp = ppc(ppr)anddp = ppcdppr.14Thisobtains cg = 1 1 dz − p pc p pr zp pc dp pr (2.19) Multiplyingthroughbythepseudocriticalpressure,theproductcg(ppc)isobtained,whichTrube definedasthepseudoreducedcompressibility(cr): cr = cg p pc = 1 1 dz − p pr z dp pr (2.20) Mattar,Brar,andAzizdevelopedananalyticalexpressionforcalculatingthepseudoreducedcompressibility.15Theexpressionis cr = 1 0.27 − 2 p pr z T pr (∂z / ∂pr )T pr 1 + ( ρr / z )(∂z / ∂ρr )T pr (2.21) TakingthederivativeofEq.(2.13),theequationofstatedevelopedbyDranchukandAbou-Kassem,10 thefollowingareobtained: ∂z ∂ 4 ∂ρ = c1 (T pr ) + 2 c2 (T pr )ρr − 5 c3 (T pr )ρr + ∂ρ [ c4 (T pr , ρr )] r r T (2.22) ∂ 2A ρ [ c4 (T pr , ρr )] = 103 r [1 + A11 ρr2 − ( A11 ρr2 )2 ] exp( − A11 ρr2 ) ∂ρr T pr (2.23) pr and UsingEqs.(2.21)to(2.23)andthedefinitionofthepseudoreducedcompressibility,thegascompressibilitycanbecalculatedforanygasaslongasthegaspressureandtemperaturearewithin therangesspecifiedfortheDranchukandAbou-Kassemcorrelation.Usingtheseequations,Blasingame,Johnston,andPoegeneratedFigs.2.4and2.5.16Inthesefigures,theproductofcrTpr is plottedasafunctionofthepseudoreducedproperties,ppr and Tpr.Example2.5illustrateshowto usethesefigures.Becausetheyarelogarithmicinnature,betteraccuracycanbeobtainedbyusing theequationsdirectly. 2.3 Review of Gas Properties Example 2.5 39 Finding Compressibility Using the Mattar, Brar, and Aziz Method Given Findthecompressibilityfora0.90specificgravitygascondensatewhenthetemperatureis150°F andpressureis4500psia. 10 , T pr ture era mp d te uce 1.4 Red 1.3 1.2 1.1 1.05 crTpr 1 0.1 0.01 Figure 2.4 0.1 1 10 Reduced pressure, ppr Variation in crTpr for natural gases for 1.05 ≤ Tpr ≤ 1.4 (after Blasingame).16 100 Chapter 2 40 • Review of Rock and Fluid Properties Solution FromEq.(2.11)and(2.12),ppc=636psiaandTpc=431°R.Thus, p pr = 4500 150 + 460 = 7.08 and T pr = = 1.42 636 431 10 CrTpr 1 0.1 Tpr 3.0 2.8 2.6 2.4 2.2 2.0 1.8 0.01 Figure 2.5 1.6 1.4 0.1 1 10 Reduced pressure, Ppr Variation in crTpr for natural gases for 1.4 ≤ Tpr ≤ 3.0 (after Blasingame).16 100 2.3 Review of Gas Properties 41 FromFig.2.5,crTpr=0.088.Thus, cr = cg = 2.3.6 cr T pr T pr = 0.088 = 0.062 1.42 cr 0.062 = = 97.5(10 )−6 psi−1 p pc 636 Viscosity The viscosity of natural gas depends on the temperature, pressure, and composition of the gas. Ithasunitsofcentipoise(cp).Itisnotcommonlymeasuredinthelaboratorybecauseitcanbe estimatedwithgoodprecision.Carr,Kobayashi,andBurrowshavedevelopedcorrelationcharts, Figs. 2.6 and 2.7, for estimating the viscosity of natural gas from the pseudoreduced temperatureandpressure.17Thepseudoreducedtemperatureandpressuremaybeestimatedfromthegas Gas gravity (air = 1.000) 1.0 1.5 .016 2.0 .0015 0 .013 400ºF .012 .011 300ºF .010 200ºF .008 100ºF .007 0 1.5 1. .0005 0 G= 0 .0015 30 35 40 45 Molecular weight 50 55 60 15 1.0 5 G .6 =0 .0005 0 0 .0010 0 25 5 10 Mol % CO2 1. .0010 5 10 Mol % N2 15 2.0 5 . 1 1.0 .0005 20 0.6 2.0 Correction added to viscocity-centipose Viscosity, at 1 atm, μ1, centipoise .014 .006 15 2. .0010 .015 G = 0.6 0 5 10 Mol % H2S 15 Figure 2.6 The viscosity of hydrocarbon gases at 1 atm and reservoir temperature, with corrections for nitrogen, carbon dioxide, and hydrogen sulfide (after Carr, Kobayashi, and Burrows, trans. AlME).17 Chapter 2 42 • Review of Rock and Fluid Properties 6.0 5.0 20 3.0 15 10 Viscosity ratio, μ/μ1 4.0 Pse udo red uce dp 8 res sur e, P pr 6 2.0 4 3 2 1 1.0 0.8 Figure 2.7 1.0 1.2 1.4 1.6 1.8 2.0 2.2 2.4 Pseudoreduced temperature, Tpr 2.6 2.8 3.0 Viscosity ratio as a function of pseudoreduced temperature and pressure (after Carr, Kobayashi, and Burrows, trans. AlME).17 specificgravityorcalculatedfromthecompositionofthegas.Theviscosityat1atmandreservoir temperature(Fig.2.6)ismultipliedbytheviscosityratio(Fig.2.7)toobtaintheviscosityatreservoirtemperatureandpressure.TheinsertsofFig.2.6arecorrectionstobeaddedtotheatmospheric viscositywhenthegascontainsnitrogen,carbondioxide,and/orhydrogensulfide.Example2.6 illustratestheuseoftheestimationcharts. Example 2.6 Using Correlation Charts to Estimate Reservoir Gas Viscosity Given Reservoirpressure=2680psia Reservoirtemperature=212°F Wellfluidspecificgravity=0.90(Air=1.00) Pseudocriticaltemperature=420°R Pseudocriticalpressure=670psia Carbondioxidecontent=5mol% 2.3 Review of Gas Properties 43 Solution μ1=0.0117cpat1atm(Fig.2.6) CorrectionforCO2=0.0003cp(Fig.2.6,insert) μ1=0.0117+0.0003=0.0120cp(correctedforCO2) T pr = 672 = 1.60 420 p pr = 2680 = 4.00 670 μ/μ1=1.60(Fig.2.7) μ=1.60×0.0120=0.0192cpat212°Fand2608psia Lee,Gonzalez,andEakindevelopedasemiempiricalmethodthatgivesanaccurateestimate ofgasviscosityformostnaturalgaseshavingspecificgravitieslessthan0.77ifthez-factorhas beencalculatedtoincludetheeffectofcontaminants.18Forthedatafromwhichthecorrelation wasdeveloped,thestandarddeviationinthecalculatedgasviscositywas2.69%.Therangesof variablesusedinthecorrelationwere100<p(psia)<8000,100<T (°F)<340,0.55<N2(mol%) <4.8,and0.90<CO2(mol%)<3.20.Inadditiontothegastemperatureandpressure,themethod requiresthez-factorandmolecularweightofthegas.Thefollowingequationsareusedinthecalculationforthegasviscosityincp: where μg=(10–4)Kexp(XρgY) K= (9.379 + 0.01607 M w )T 1.5 (209.2 + 19.26 M w + T ) X = 3.448 + 986.4 + 0.01009 M w T Y=2.447–0.2224X where ρg=gasdensityfromEq.(2.5),g/cc p = pressure, psia T=temperature,°R Mw=gasmolecularweight (2.24) (2.24a) (2.24b) (2.24c) 44 2.4 Chapter 2 • Review of Rock and Fluid Properties Review of Crude Oil Properties Thenextfewsectionscontaininformationoncrudeoilproperties,includingseveralcorrelations that can be used to estimate values for the properties. McCain, Spivey, and Lenn present an excellent review of these correlations in their book, Reservoir Fluid Property Correlations.19 However,thesecrudeoilpropertycorrelationsare,ingeneral,notasreliableasthecorrelations thathavebeenpresentedearlierforgases.Therearetwomainreasonsfortheoilcorrelations beinglessreliable.Thefirstisthatoilsusuallyconsistofmanymorecomponentsthangases. Whereasgasesaremostlymadeupofalkanes,oilscanbemadeupofseveraldifferentclassesof compounds(e.g.,aromaticsandparaffins).Thesecondreasonisthatmixturesofliquidcomponentsexhibitmorenonidealitiesthanmixturesofgascomponents.Thesenonidealitiescanlead toerrorsinextrapolatingcorrelationsthathavebeendevelopedforacertaindatabaseofsamples toparticularapplicationsoutsidethedatabase.Beforeusinganyofthecorrelations,theengineer shouldmakesurethattheapplicationofinterestfitswithintherangeofparametersforwhich acorrelationwasdeveloped.Aslongasthisisdone,thecorrelationsusedforestimatingliquid propertieswillbeadequateandcanbeexpectedtoyieldaccurateresults.Correlationsshould onlybeusedintheearlystagesofproductionfromareservoirwhenlaboratorydatamaynot beavailable.Themostaccuratevaluesforliquidpropertieswouldcomefromlaboratorymeasurementsonabottom-holefluidsample.Ezekwehaspresentedasummaryofvariousmethods usedtocollectreservoirfluidsamplesandsubsequentlaboratoryprocedurestomeasurefluid properties.3 2.4.1 Solution Gas-Oil Ratio, Rso The amount of gas dissolved in an oil at a given pressure and temperature is referred to as the solution gas-oil ratio (Rso),inunitsofSCF/STB.Thesolubilityofnaturalgasincrudeoildepends onthepressure,temperature,andcompositionofthegasandthecrudeoil.Foraparticulargasand crudeoilatconstanttemperature,thequantityofsolutiongasincreaseswithpressure,andatconstantpressure,thequantitydecreaseswithincreasingtemperature.Foranytemperatureandpressure,thequantityofsolutiongasincreasesasthecompositionsofthegasandcrudeoilapproach each other—that is, it will be greater for higher specific gravity gases and higherAPI gravity crudes.Unlikethesolubilityof,say,sodiumchlorideinwater,gasisinfinitelysolubleincrudeoil, thequantitybeinglimitedonlybythepressureorbythequantityofgasavailable. Crudeoilissaidtobesaturatedwithgasatanypressureandtemperatureif,onaslightreductioninpressure,somegasisreleasedfromthesolution.Conversely,ifnogasisreleasedfrom thesolution,thecrudeoilissaidtobeundersaturatedatthatpressure.Theundersaturatedstate impliesthatthereisadeficiencyofgaspresentandthat,hadtherebeenanabundanceofgaspresent,theoilwouldbesaturatedatthatpressure.Theundersaturatedstatefurtherimpliesthatthere isnofreegasincontactwiththecrudeoil(i.e.,thereisnogascap). Gassolubilityunderisothermalconditionsisgenerallyexpressedintermsoftheincreasein solutiongasperunitofoilperunitincreaseinpressure(e.g.,SCF/STB/psiordRso/dp).Although formanyreservoirs,thissolubilityfigureisapproximatelyconstantoveraconsiderablerangeof 2.4 Review of Crude Oil Properties 45 pressures,forprecisereservoircalculations,thesolubilityisexpressedintermsofthetotalgasin solutionatanypressure(e.g.,SCF/STB,orRso).Itwillbeshownthatthereservoirvolumeofcrude oilincreasesappreciablybecauseofthesolutiongas,andforthisreason,thequantityofsolution gasisusuallyreferencedtoaunitofstock-tankoilandthesolution gas-oil ratio (Rso)isexpressed instandardcubicfeetperstock-tankbarrel.Figure2.8showsthevariationofsolutiongaswith pressurefortheBigSandyreservoirfluidatreservoirtemperature160°F.Attheinitialreservoir pressureof3500psia,thereis567SCF/STBofsolutiongas.Thegraphindicatesthatnogasis evolvedfromthesolutionwhenthepressuredropsfromtheinitialpressureto2500psia.Thusthe oilisundersaturatedinthisregion,andtherecanbenofreegasphase(gascap)inthereservoir. Thepressure2500psiaiscalledthebubble-point pressure,foratthispressurebubblesoffreegas firstappear.At1200psia,thesolutiongasis337SCF/STB,andtheaveragesolubilitybetween 2500and1200psiais Averagesolubility = 567 − 337 = 0.177 SCF/ST TB/psi 2500 − 1200 ThedataofFig.2.8wereobtainedfromalaboratoryPVTstudyofabottom-holesampleoftheBig SandyreservoirfluidusingaflashliberationprocessthatwillbedefinedinChapter7. 600 567 SCF/STB At 1200 psia RS = 337 300 200 Initial pressure 400 Bubble-point pressure Solution gas, SCF/STB 500 100 0 0 Figure 2.8 500 1000 1500 2000 Pressure, psia 2500 3000 3500 Solution gas-oil ratio of the Big Sandy Field reservoir oil, by flash liberation at reservoir temperature of 160°F. Chapter 2 46 • Review of Rock and Fluid Properties InChapter7,itwillbeshownthatthesolutiongas-oilratioandotherfluidpropertiesdepend onthemannerbywhichthegasisliberatedfromtheoil.Thenatureofthephenomenonisdiscussed togetherwiththecomplicationsitintroducesintocertainreservoircalculations.Forthesakeofsimplicity,thisphenomenonisignoredandastock-tankbarrelofoilisidentified,withabarrelofresidual oilfollowingaflashliberationprocess,andthesolutiongas-oilratiosbyflashliberationareused. Estimatingavalueforthesolutiongas-oilratio,Rsob,atthebubblepointrequiresinformation abouttheconditionsatwhichthesurfaceseparatorisoperating.Iftheseparatorpressureandtemperaturearenotavailable,thenValkoandMcCainproposethefollowingequationtoestimateRsob20: Rsob = 1.1618 Rso,SP (2.25) where Rso,SP = solution gas-oil ratio at the exit of the separator Whenlaboratoryanalysesofthereservoirfluidsarenotavailable,itisoftenpossibletoestimatethesolutiongas-oilratiowithreasonableaccuracy.Velarde,Blasingame,andMcCaingive acorrelationmethodfromwhichthesolutiongas-oilratiomaybeestimatedfromthereservoir pressure,thereservoirtemperature,thebubble-pointpressure,thesolutiongas-oilratioatthebubble-pointpressure,theAPIgravityofthetankoil,andthespecificgravityoftheseparatorgas.21 Thecorrelationinvolvesthefollowingequations: Rso = ( Rsob )( Rsor ) (2.26) Rsor = a1 pra2 + (1 − a1 ) pra3 (2.26a) pr = ( p − 14.7 ) / ( pb − 14.7 ) (2.26b) 0.247235 a1 = 9.73(10 −7 )γ 1g.,672608 ρ00,.929870 ( pb − 14.7 )1.056052 SP API T (2.26c) .004750 0.337711 0.132795 a2 = 0.022339γ g−,1SP ρ0, API T ( pb − 14.7 )0.302065 (2.26d) .485480 −0.164741 −0.091330 a3 = 0.725167γ g−,1SP ρ0, API T ( pb − 14.7 )0.047094 (2.26e) where Rsob=solutiongas-oilratioatthebubble-pointpressure,STB/SCF p=pressure,psia pb =pressureatthebubble-point,psia γg,SP=specificgravityoftheseparatorgas ρo,API=gravityofthestock-tankoil,°API 2.4 Review of Crude Oil Properties 47 T=temperature,°F Thegravityofthestock-tankoilisfrequentlyreportedasaspecificgravityrelativetowaterat60°F. Theequationusedtoconvertfromspecificgravitytounitsof°APIis °API = 141.5 − 131.5 γo (2.27) Ifthedensityisreportedin°APIandisneededinlb/ft3,thenrearrangeEq.(2.27)andsolveforthe specific gravity.The specific gravity is then multiplied by the density of water at 60°F, which is 62.4lb/ft3. 2.4.2 Formation Volume Factor, Bo Theformation volume factor(Bo),whichisalsoabbreviatedFVF,atanypressuremaybedefined asthevolumeinbarrelsthatonestock-tankbarreloccupiesintheformation(reservoir)atreservoir temperature,withthesolutiongasthatcanbeheldintheoilatthatpressure.Becauseboththe temperatureandthesolutiongasincreasethevolumeofthestock-tankoil,thefactorwillalwaysbe greaterthan1.Whenallthegaspresentisinsolutionintheoil(i.e.,atthebubble-pointpressure), afurtherincreaseinpressuredecreasesthevolumeataratethatdependsonthecompressibilityof theliquid. Itwasobservedearlierthatthesolutiongascausesaconsiderableincreaseinthevolumeof thecrudeoil.Figure2.9showsthevariationintheformationvolumefactorofthereservoirliquid oftheBigSandyreservoirasafunctionofpressureatreservoirtemperatureof160°F.Becauseno gasisreleasedfromsolutionwhenthepressuredropsfromtheinitialpressureof3500psiatothe bubble-pointpressureat2500psia,thereservoirfluidremainsinasingle(liquid)state;however, becauseliquidsareslightlycompressible,theFVFincreasesfrom1.310bbl/STBat3500psiato 1.333bbl/STBat2500psia.Below2500psia,thisliquidexpansioncontinuesbutismaskedby amuchlargereffect:thedecreaseintheliquidvolumeduetothereleaseofgasfromsolution.At 1200psia,theFVFdecreasesto1.210bbl/STB,andatatmosphericpressureand160°F,theFVF decreasesto1.040bbl/STB.Thecoefficientoftemperatureexpansionforthe30°APIstock-tank oiloftheBigSandyreservoiriscloseto0.0004perdegreesFahrenheit;therefore,onestock-tank barrelat60°Fwillexpandtoabout1.04bblat160°F,ascalculatedfrom VT = V60[1+β(T–60)] (2.28) V160=1.00[1+0.00040(160–60)]=1.04bbl whereβisthetemperaturecoefficientofexpansionoftheoil. Oneobviousimplicationoftheformationvolumefactoristhatforevery1.310bblofreservoirliquidintheBigSandyreservoir,only1.000bbl,or76.3%,canreachthestocktank.This Chapter 2 48 • Review of Rock and Fluid Properties 3500 psia BO = 1.31 2500 psia BOB = 1.333 1.30 1200 psia BO = 1.21 1.20 1.10 1.00 Figure 2.9 14.7 psia & 160ºF BO = 1.04 14.7 psia & 60ºF BO = 1.00 0 500 1000 1500 2000 Pressure, psia 2500 Initial pressure Bubble point pressure Formation volume factor, bbl/STB 1.40 3000 3500 Formation volume factor of the Big Sandy Field reservoir oil, by flash liberation at reservoir temperature of 160°F. figure(76.3%or0.763)isthereciprocaloftheformationvolumefactorandiscalledtheshrinkage factor.Justastheformationvolumefactorismultipliedbythestock-tankvolumetofindthe reservoirvolume,theshrinkagefactorismultipliedbythereservoirvolumetofindthestock-tank volume.Althoughbothtermsareinuse,petroleumengineershavealmostuniversallyadoptedthe formationvolumefactor.Asmentionedpreviously,theformationvolumefactorsdependonthe typeofgasliberationprocess—aphenomenonthatweignoreuntilChapter7. Insomeequations,itisconvenienttousethetermtwo-phase formation volume factor(Bt), whichisdefinedasthevolumeinbarrelsonestock-tankbarreland its initial complement of dissolved gasoccupiesatanypressureandreservoirtemperature.Inotherwords,itincludestheliquid volume,Bo,plusthevolumeofthedifferencebetweentheinitialsolutiongas-oilratio,Rsoi,andthe solutiongas-oilratioatthespecifiedpressure,Rso.IfBgisthegasvolumefactorinbarrelsperstandardcubicfootofthesolutiongas,thenthetwo-phaseformationvolumefactorcanbeexpressedas Bt = Bo + Bg(Rsoi – Rso) (2.29) Abovethebubblepoint,pressureRsoi = Rsoandthesingle-phaseandtwo-phasefactorsareequal. Belowthebubblepoint,however,whilethesingle-phasefactordecreasesaspressuredecreases,the two-phasefactorincreases,owingtothereleaseofgasfromsolutionandthecontinuedexpansion ofthegasreleasedfromsolution. Thesingle-phaseandtwo-phasevolumefactorsfortheBigSandyreservoirfluidmaybe visualizedbyreferringtoFig.2.10,whichisbasedondatafromFigs.2.8and2.9.Figure2.10 2.4 Review of Crude Oil Properties 49 pA pA p p01 ~ ~ pB ~ ~ ~ ~ ~ ~ Free gas 2.99 ft3 Free gas 676 ft3 Free gas 567 ft3 1.31 bbl 1.333 bbl 1.21 bbl 1.04 bbl 1.0 bbl p01 = 3500 psia T01 = 160ºF A pB = 2500 psia T01 = 160ºF B p = 1200 psia T01 = 160ºF C pA = 14.7 psia T01 = 160ºF D pA = 14.7 psia T = 60ºF E Figure 2.10 Visual conception of the change in single-phase and in two-phase formation volume factors for the Big Sandy reservoir fluid. (A)showsacylinderfittedwithapistonthatinitiallycontains1.310bbloftheinitialreservoir fluid (liquid) at the initial pressure of 3500 psia and 160°F.As the piston is withdrawn, the volumeincreasesandthepressureconsequentlymustdecrease.At2500psia,whichisthebubble-pointpressure,theliquidvolumehasexpandedto1.333bbl.Below2500psia,agasphase appearsandcontinuestogrowasthepressuredeclines,owingtothereleaseofgasfromsolution andtheexpansionofgasalreadyreleased;conversely,theliquidphaseshrinksbecauseoflossof solutiongasto1.210bblat1200psia.At1200psiaand160°F,theliberatedgashasadeviation factorof0.890,andthereforethegasvolumefactorwithreferencetostandardconditionsof14.7 psiaand60°Fis Bg = znR ' T 0.890 × 10.73 × 620 = p 379.4 × 1200 =0.01300ft3/SCF =0.002316bbl/SCF Figure2.8showsaninitialsolutiongasof567SCF/STBand,at1200psia,337SCF/STB,the differenceof230SCFbeingthegasliberateddownto1200psia.Thevolumeofthese230 SCFis Vg=230×0.01300=2.990ft3 Thisfreegasvolume,2.990ft3or0.533bbl,plustheliquidvolume,1.210bbl,isthetotalFVFor 1.743bbl/STB—thetwo-phasevolumefactorat1200psia.ItmayalsobeobtainedbyEq.(2.28)as Bt=1.210+0.002316(567–337) Chapter 2 50 • Review of Rock and Fluid Properties =1.210+0.533=1.743bbl/STB Figure2.10(C)showstheseseparateandtotalvolumesat1200psia.At14.7psiaand160°F(D), thegasvolumehasincreasedto676ft3andtheoilvolumehasdecreasedto1.040bbl.Thetotal liberatedgasvolume,676ft3at160°Fand14.7psia,isconvertedtostandardcubicfeetat60°F and14.7psiausingtheidealgaslaw,producing567SCF/STBasshownin(E).Correspondingly, 1.040bblat160°Fisconvertedtostock-tankconditionsof60°FasshowninEq.(2.28)togive 1.000STB,alsoshownin(E). Thesingle-phaseformationvolumefactorforpressureslessthanthebubble-pointpressuremay beestimatedfromthesolutiongas-oilratio,oildensity,densityofthestock-tankoil,andtheweighted averagespecificgravityofthesurfacegas,usingacorrelationpreparedbyMcCain,Spivey,andLenn:19 Bo = ρo, ST + 0.01357 Rsoγ g , S where (2.30) ρo ρo,ST =densityofstock-tankoil,lb/ft3 γg,S=weightedaveragespecificgravityofthesurfacegas ρo=oildensity Theweightedaveragespecificgravityofthesurfacegasshouldbecalculatedfromthespecific gravitiesofthestock-tankandtheseparatorgasesfromthefollowingequation: Table 2.2 Relative Volume Data a (1) Pressure (psig) (2) Relative volume factorsa (Vr ) 5000 0.9739 4700 0.9768 4400 0.9799 4100 0.9829 3800 0.9862 3600 0.9886 3400 0.9909 3200 0.9934 3000 0.9960 2900 0.9972 2800 0.9985 2695 1.0000 Vr=volumerelativetothevolumeatthebubble-pointpressure 2.4 Review of Crude Oil Properties γ g ,S = 51 γ g,SP RSP + γ g,ST RST RSP + RST (2.31) where γg,SP=specificgravityoftheseparatorgas RSP=separatorgas-oilratio γg,ST=specificgravityofthestock-tankgas RST=stock-tankgas-oilratio Forpressuresgreaterthanthebubble-pointpressure,Eq.(2.32)isusedtocalculatetheformationvolumefactor: where Bo = Bobexp[co(pb – p)] (2.32) Bob=oilformationvolumefactoratthebubble-pointpressure co=oilcompressibility,psi–1 Column(2)ofTable2.2showsthevariationinthevolumeofareservoirfluidrelativetothe volumeatthebubblepointof2695psig,asmeasuredinthelaboratory.Theserelativevolumefactors maybeconvertedtoformationvolumefactorsiftheformationvolumefactoratthebubblepointis known.Forexample,ifBob=1.391bbl/STB,thentheformationvolumefactorat4100psigis Boat4100psig=1.391(0.9829)=1.367bbl/STB 2.4.3 Isothermal Compressibility Sometimesitisdesirabletoworkwithvaluesoftheliquidcompressibilityratherthantheformationorrelativevolumefactors.Theisothermalcompressibility,orthebulkmodulusofelasticityof aliquid,isdefinedbyEq.(2.1): c=− 1 dV V dp (2.1) Thecompressibility,c,iswritteningeneraltermssincetheequationappliesforbothliquidsand solids.Foraliquidoil,cwillbegivenasubscriptofcotodifferentiateitfromasolid.Because dV/dp is a negative slope, the negative sign converts the oil compressibility, co, into a positive number.BecausethevaluesofthevolumeVandtheslopeofdV/dparedifferentateachpressure, theoilcompressibilityisdifferentateachpressure,beinghigheratthelowerpressure.Averageoil compressibilitiesmaybeusedbywritingEq.(2.1)as Chapter 2 52 co = − • Review of Rock and Fluid Properties 1 (V1 − V2 ) × V ( p1 − p2 ) (2.33) ThereferencevolumeVinEq.(2.33)maybeV1, V2,oranaverageofV1 and V2.Itiscommonly reportedforreferencetothesmallervolume—thatis,thevolumeatthehigherpressure.ThefollowingexpressionsdeterminetheaveragecompressibilityofthefluidofTable2.2between5000 psigand4100psig co = 0.9829 − 0.9739 = 10.27 × 10 −6 pssi−1 0.9739 (5000 − 4100 ) between4100psigand3400psig co = 0.9909 − 0.9829 = 11.63 × 10 −6 pssi−1 0.9829 ( 4100 − 3400 ) andbetween3400psigand2695psig co = 1.0000 − 0.9909 = 13.03 × 10 −6 pssi−1 0.9909 ( 3400 − 2695 ) Acompressibilityof13.03×10–6 psi–1meansthatthevolumeof1millionbarrelsofreservoirfluidwillincreaseby13.03bblsforareductionof1psiinpressure.Thecompressibilityof undersaturatedoilsrangesfrom5to100×10–6 psi–1,beinghigherforthehigherAPIgravities,for thegreaterquantityofsolutiongas,andforhighertemperatures. Spivey,Valko, and McCain presented a correlation for estimating the compressibility for pressuresabovethebubble-pointpressure.22Thiscorrelationyieldsthecompressibilityinunitsof microsips(1microsip=10–6/psi).Thecorrelationinvolvesthefollowingequations: lnco=2.434+0.475Z+0.048Z2–ln(106) (2.34) Z = ∑ n =1 Z n (2.34a) Z1 = 3.011 − 2.6254 ln( ρo, API ) + 0.497[ln( ρo, API )]2 (2.34b) Z 2 = −0.0835 − 0.259 ln(γ g,SP ) + 0.382[ln(γ g,SP )]2 (2.34c) 6 2.4 Review of Crude Oil Properties 53 Z 3 = 3.51 − 0.0289 ln( ρb ) − 0.0584[ln( pb )]2 p p Z 4 = 0.327 − 0.608 ln + 0.0911 ln pb pb (2.34d) 2 (2.34e) Z 5 = −1.918 − 0.642 ln( Rsob ) + 0.154[ln( Rsob )]2 (2.34f) Z 6 = 2.52 − 2.73ln(T ) + 0.429[ ln(T )]2 (2.34g) Thecorrelationgivesgoodresultsforthefollowingrangesofdata: 11.6≤ ρo,API ≤57.7°API 0.561≤ γg,SP ≤1.798(air=1) 120.7≤ pb ≤6658.7psia 414.7≤ p ≤8114.7psia 12≤ Rsob ≤1808SCF/STB 70.7≤ T ≤320°F 3.6≤ co ≤50.3microsips Villena-Lanzidevelopedacorrelationtoestimatecoforblackoils.23Ablackoilhasnearlyall itsdissolvedgasremoved.Thecorrelationisgoodforpressuresbelowthebubble-pointpressure andisgivenby ln(co)=–0.664–1.430ln(p)–0.395ln(pb)+0.390ln(T) +0.455ln(Rsob)+0.262ln(ρo,API) where T = °F Thecorrelationwasdevelopedfromadatabasecontainingthefollowingranges: 31.0(10)–6<co(psia–1)<6600(10)–6 500<p(psig)<5300 763<pb(psig)<5300 78<T (°F)<330 1.5<Rsob,gas-oilratio(SCF/STB)<1947 6.0<ρo,API(°API)<52.0 0.58<γg<1.20 (2.35) Chapter 2 54 • Review of Rock and Fluid Properties 8 7 6 A B.P. Viscosity, cp 5 4 3 B B.P. 2 B.P. C 1 B.P. D 0 0 1000 2000 3000 Pressure, psig Figure 2.11 2.4.4 The viscosity of four crude oil samples under reservoir conditions. Viscosity Theviscosityofoilunderreservoirconditionsiscommonlymeasuredinthelaboratory.Figure 2.11 shows the viscosities of four oils at reservoir temperature, above and below bubble-point pressure.Belowthebubblepoint,theviscositydecreaseswithincreasingpressureowingtothe thinningeffectofgasenteringsolution,butabovethebubblepoint,theviscosityincreaseswith increasingpressure. 2.4 Review of Crude Oil Properties 55 Whenitisnecessarytoestimatetheviscosityofreservoiroils,correlationshavebeendevelopedforbothaboveandbelowthebubble-pointpressure.Egbogahpresentedacorrelation thatisaccuratetoanaverageerrorof6.6%for394differentoils.24Thecorrelationisforwhat isreferredtoas“dead”oil,whichsimplymeansitdoesnotcontainsolutiongas.Asecond correlationisusedinconjunctionwiththeEgbogahcorrelationtoincludetheeffectofsolutiongas.Egbogah’scorrelationfordeadoilatpressureslessthanorequaltothebubble-point pressureis log10[log10(μod+1)]=1.8653–0.025086ρo,API–0.5644log(T) (2.36) where μod=deadoilviscosity,cp T=temperature,°F Thecorrelationwasdevelopedfromadatabasecontainingthefollowingranges: 59<T(°F)<176 –58<pourpoint,Tpour(°F)<59 5.0<ρo,API(°API)<58.0 BeggsandRobinson25,26developedtheliveoilviscositycorrelationthatisusedinconjunctionwiththedeadoilcorrelationgiveninEq.(2.36)tocalculatetheviscosityofoilsatandbelow thebubblepoint: B μo = Aμod (2.37) where A=10.715(Rso+100)–0.515 B=5.44(Rso+150)–0.338 TheaverageabsoluteerrorfoundbyBeggsandRobinsonwhileworkingwith2073oilsampleswas 1.83%.Theoilsamplescontainedthefollowingranges: 0<p(psig)<5250 70<T(°F)<295 20<Rso,gas-oilratio(SCF/STB)<2070 16<ρo,API(°API)<58 Chapter 2 56 • Review of Rock and Fluid Properties For pressures above the bubble point, the oil viscosity can be estimated by the following correlationdevelopedbyPetroskyandFarshad:27 μo = μob + 1.3449(10 −3 )( p − pb )10 A (2.38) where A = −1.0146 + 1.3322[log( μob )] − 0.4876[log(μob )]2 − 1.15036[log( μob )]3 and μob=oilviscosityatthebubble-pointpressure,cp Thefollowingexampleproblemillustratestheuseofthecorrelationsthathavebeenpresentedfor thevariousoilproperties. Example 2.7 Using Correlations to Estimate Values for Liquid Properties at Pressures of 2000 psia and 4000 psia Given T=180°F pb=2500psia Rso,SP = 664 SCF/STB γg,SP=0.56 γg,S=0.60 ρo,API=40°API ρo,b =39.5lb/ft3 ρo,2000 =41.6lb/ft3 γo=0.85 Solution Solution Gas-Oil Ratio, Rso p=4000psia(p > pb) Forpressuresgreaterthanthebubble-pointpressure,Rso = Rsob;therefore,fromEq.(2.25), Rso = Rsob=1.1618 Rso,SP=1.1618(664) Rsob=771SCF/STB 2.4 Review of Crude Oil Properties 57 p=2000psia(p<pb) Rso=(Rsob)(Rsor)=771Rsor Rsor = a1 pra2 + (1 − a1 ) pra3 pr=(p–14.7)/(pb–14.7)=(2000–14.7)/(2500–14.7)=0.799 0.247235 a1 = 9.73(10 −7 )γ 1g.,672608 ρ00,.929870 ( pb − 14.7 )1.056052 SP API T a1=9.73(10–7)0.561.672608400.9298701800.247235(2500–14.7)1.056052=0.158 .004750 0.337711 0.132795 a2 = 0.022339γ g−,1SP ρ0, API T ( pb − 14.7 )0.302065 a2=0.022339(0.56–1.004750)400.3377111800.132795(2500–14.7)0.302065=2.939 .485480 −0.164741 −0.091330 a3 = 0.724167γ g−,1SP ρ0, API T ( pb − 14.7 )0.047094 a3=0.725167(0.56–1.485480)40–0.164741180–0.091330(2500–14.7)0.047094=0.840 Rsor=0.288(0.799)0.194+(1–0.288)(0.799)0.495=0.779 Rso=(771)(0.779)=601 Isothermal Compressibility, co FromEq.(2.34), p=4000psia(p > pb) ln co=2.434+0.475Z+0.048Z2–ln(106) Z = ∑ n =1 Z 6 n Z1=3.011–2.6254ln(ρo,API)+0.497[ln(ρo,API)]2 Z1=3.011–2.6254ln(40)+0.497[ln(40)]2=0.089 Z2=–0.0835–0.259ln(γg,SP)+0.382[ln(γg,SP)]2 Z2=–0.0835–0.259ln(0.56)+0.382[ln(0.56)]2=0.195 Chapter 2 58 • Review of Rock and Fluid Properties Z3=3.51–0.0289ln(pb)–0.0584[ln(pb)]2 Z3=3.51–0.0289ln(2500)–0.0584[ln(2500)]2=–0.291 p p Z 4 = 0.327 − 0.608 ln + 0.0911[ln ]2 pb pb Z4=0.327–0.608ln(4000/2500)+0.0911[ln(4000/2500)]2=0.061 Z5=–1.918–0.642ln(Rsob)+0.154[ln(Rsob)]2 Z5=–1.918–0.642ln(771)+0.154[ln(771)]2=0.620 Z6=2.52–2.73ln(T)+0.429[ln(T)]2 Z6=2.52–2.73ln(180)+0.429[ln(180)]2=–0.088 Z = ∑ n =1 Z n = 0.089 + 0.195 + ( −0.291) + 0.061 + 0.620 + ( −0.088 ) = 0.586 6 ln(co)=ln(co)=2.434+0.475Z+0.048Z2–ln(106)=2.434 +0.475(0.586)+0.048(0.586)2–13.816=–11.087 co=15.3(10)–6 psi–1 p=2000psia(p<pb) FromEq.(2.35), ln(co)=–0.664–1.430ln(p)–0.395ln(pb)+0.390ln(T) +0.455ln(Rsob)+0.262ln(ρo,API) ln(co)=–0.664–1.430ln(2000)–0.395ln(2500)+0.390ln(180) +0.455ln(771)+0.262ln(40) co=183(10)–6 psi–1 Formation Volume Factor, Bo p=4000psia(p > pb) 2.4 Review of Crude Oil Properties 59 FromEq.(2.32), Bo = Bobexp[co(pb – p)] BobiscalculatedfromEq.(2.30)atthebubble-pointpressure: Bob = γ o,ST = ρo,ST + 0.01357 Rsoγ g,S ρo,b 141.5 141.5 = = 0.825 ρo, API + 131.5 40 + 131.5 ρo,ST = γ o,ST (62.4 ) = 51.5 Bob = 51.5 + 0.01357( 771)(0.60 ) 39.5 Bob =1.463bbl/STB Bo=1.463exp[15.3(10)–6(2500–4000)]=1.430bbl/STB p=2000psia(p<pb) FromEq.(2.30), Bo = Bo = ρo,ST + 0.01357 Rsoγ g,S ρo 51.5 + 0.01357(601)(0.60 ) 41.6 Bo=1.356bbl/STB Viscosity, μo FromEq.(2.36), log10[log10(μobd+1)]=1.8653–0.025086ρo,API–0.5644log(T) log10[log10(μobd+1)]=1.8653–0.025086(40)–0.5644log(180) Chapter 2 60 FromEq.(2.37), • Review of Rock and Fluid Properties μobd=1.444cp B μob = Aμobd A =10.715(Rsob +100)–0.515=10.715(771+100)–0.515=0.328 B =5.44(Rsob +150)–0.338=5.44(771+150)–0.338=0.542 μob =0.328(1.444)0.542=0.400cp p =2000psia(p < pb) FromEq.(2.36),μodwillbethesameasμobd: μobd = 1.444cp B μo = Aμobd A =10.715(Rso +100)–0.515=10.715(601+100)–0.515=0.367 B =5.44(Rso +150)–0.338=5.44(601+150)–0.338=0.580 μo =0.367(1.444)0.580=0.454cp FromEq.(2.38), p=4000psia(p > pb) μo = μob + 1.3449(10 −3 )( p − pb )10 A where A=–1.0146+1.3322[log(μob)]–0.4876[log(μob)]2–1.15036[log(μob)]3 A=–1.0146+1.3322[log(0.400)]–0.4876[log(0.400)]2–1.15036[log(0.400)]3 A = –1.549 μo=0.400+1.3449(10–3)(4000–2500)10–1.549=0.457cp 2.5 Review of Reservoir Water Properties 2.5 61 Review of Reservoir Water Properties Thepropertiesofformationwatersareaffectedbytemperature,pressure,andthequantityofsolutiongasanddissolvedsolids,buttoamuchsmallerdegreethancrudeoils.Thecompressibility oftheformation,orconnate,watercontributesmateriallyinsomecasestotheproductionofvolumetricreservoirsabovethebubblepointandaccountsformuchofthewaterinfluxinwater-drive reservoirs.Whentheaccuracyofotherdatawarrantsit,thepropertiesoftheconnatewatershould beenteredintothematerial-balancecalculationsonreservoirs.Thefollowingsectionscontaina numberofcorrelationsadequateforuseinengineeringapplications. 2.5.1 Formation Volume Factor McCain28developedthefollowingcorrelationforthewaterformationvolumefactor,Bw(bbl/STB): where Bw=(1+ΔVwt)(1+ΔVwp) (2.39) ΔVwt=–1.00010×10–2+1.33391×10–4 T+5.50654×10–7 T2 ΔVwp=–1.95301×10–9 pT–1.72834×10–13 p2T–3.58922×10–7 p–2.25341×10–10 p2 T=temperature,°F p=pressure,psia Forthedatausedinthedevelopmentofthecorrelation,thecorrelationwasfoundtobeaccurateto within2%.Thecorrelationdoesnotaccountforthesalinityofnormalreservoirbrinesexplicitly, butMcCainobservedthatvariationsinsalinitycausedoffsettingerrorsinthetermsΔVwt and ΔVwp. Theoffsettingerrorscausethecorrelationtobewithinengineeringaccuracyfortheestimationof theBwofreservoirbrines. 2.5.2 Solution Gas-Water Ratio McCainhasalsodevelopedacorrelationforthesolutiongas-waterratio,Rsw(SCF/STB).28The correlationis −0.285854 Rsw ) = 10 ( −0.0840655 S T Rswp where S=salinity,%byweightsolids T=temperature,°F Rswp=solutiongastopurewaterratio,SCF/STB (2.40) Chapter 2 62 • Review of Rock and Fluid Properties RswpisgivenbyanothercorrelationdevelopedbyMcCainas Rswp = A + Bp +Cp2 (2.41) where A=8.15839–6.12265×10–2 T+1.91663×10–4 T2–2.1654×10–7 T3 B=1.01021×10–2–7.44241×10–5 T+3.05553×10–7 T2–2.94883×10–10 T3 C=–10–7(9.02505–0.130237T+8.53425×10–4 T2–2.34122×10–6 T3+2.37049×10–9 T4) T=temperature,°F ThecorrelationofEq.(2.40)wasdevelopedforthefollowingrangeofdataandfoundtobewithin 5%ofthepublisheddata: 1000<p(psia)<10,000 100<T(°F)<340 Equation(2.41)wasdevelopedforthefollowingrangeofdataandfoundtobeaccuratetowithin 3%ofpublisheddata: 0<S(%)<30 70<T(°F)<250 2.5.3 Isothermal Compressibility Osifdevelopedacorrelationforthewaterisothermalcompressibility,cw,forpressuresgreaterthan thebubble-pointpressure.29Theequationis cw = − 1 ∂Bw 1 = Bw ∂p T [ 7.033 p + 541.CNaCl − 537.0T + 403, 300 ] where CNaCl=salinity,gNaCl/liter T=temperature,°F Thecorrelationwasdevelopedforthefollowingrangeofdata: 1000<p(psig)<20,000 (2.42) 2.5 Review of Reservoir Water Properties 0<CNaCl(gNaCl/liter)<200 200<T(°F)<270 63 Thewaterisothermalcompressibilityisstronglyaffectedbythepresenceoffreegas.Therefore, McCainproposedusingthefollowingexpressionforestimatingcwforpressuresbeloworequalto thebubble-pointpressure:28 cw = − Bg ∂Rswp 1 ∂Bw + Bw ∂p T Bw ∂p T (2.43) Thefirsttermontheright-handsideofEq.(2.43)issimplytheexpressionforcwinEq.(2.42).The secondtermontheright-handsideisfoundbydifferentiatingEq.(2.41)withrespecttopressure,or ∂Rswp ∂p = B + 2Cp T whereB and CaredefinedinEq.(2.41). InproposingEq.(2.43),McCainsuggestedthatBgshouldbeestimatedusingagaswithagas gravityof0.63,whichrepresentsagascomposedmostlyofmethaneandasmallamountofethane. McCaincouldnotverifythisexpressionbycomparingcalculatedvaluesofcwwithpublisheddata, sothereisnoguaranteeofaccuracy.ThissuggeststhatEq.(2.43)shouldbeusedonlyforgross estimationsofcw. 2.5.4 Viscosity Theviscosityofwaterincreaseswithdecreasingtemperatureandingeneralwithincreasingpressureandsalinity.Pressurebelowabout70°Fcausesareductioninviscosity,andsomesalts(e.g., KCl)reducetheviscosityatsomeconcentrationsandwithinsometemperatureranges.Theeffect ofdissolvedgasesisbelievedtocauseaminorreductioninviscosity.McCaindevelopedthefollowingcorrelationforwaterviscosityatatmosphericpressureandreservoirtemperature28: where μw1 = ATB (2.44) A=109.574–8.40564S+0.313314S2+8.72213×10–3 S3 B=1.12166+2.63951×10–2 S–6.79461×10–4 S2–5.47119×10–5 S3+1.55586×10–6 S4 T=temperature,°F S=salinity,%byweightsolids Equation(2.44)wasfoundtobeaccuratetowithin5%overthefollowingrangeofdata: Chapter 2 64 • 100<T (°F)<400 0<S(%)<26 Review of Rock and Fluid Properties Thewaterviscositycanbeadjustedtoreservoirpressurebythefollowingcorrelation,againdevelopedbyMcCain:28 μw =0.9994+4.0295(10)–5p+3.1062(10)–9p2 μw1 (2.45) Thiscorrelationwasfoundtobeaccuratetowithin4%forpressuresbelow10,000psiaandwithin 7%forpressuresbetween10,000psiaand15,000psia.Thetemperaturerangeforwhichthecorrelationwasdevelopedwasbetween86°Fand167°F. 2.6 Summary Thecorrelationspresentedinthischapterarevalidforestimatingproperties,providedtheparametersfallwithinthespecifiedrangesfortheparticularpropertyinquestion.Thecorrelationswere presentedintheformofequationstofacilitatetheirimplementationintocomputerprograms. Problems 2.1 Calculatethevolume1lb-molofidealgaswilloccupyat (a) (b) (c) (d) 14.7psiaand60°F 14.7psiaand32°F 14.7psiaplus10ozand80°F 15.025psiaand60°F 2.2 A500-ft3tankcontains10lbofmethaneand20lbofethaneat90°F. (a) (b) (c) (d) Howmanymolesareinthetank? Whatisthepressureofthetankinpsia? Whatisthemolecularweightofthemixture? Whatisthespecificgravityofthemixture? 2.3 Whatarethemolecularweightandspecificgravityofagasthatisone-thirdeachofmethane,ethane,andpropanebyvolume? 2.4 A10-lbblockofdryiceisplacedina50-ft3tankthatcontainsairatatmosphericpressure 14.7psiaand75°F.Whatwillbethefinalpressureofthesealedtankwhenallthedryicehas evaporatedandcooledthegasto45°F? Problems 65 2.5 Aweldingapparatusforadrillingrigusesacetylene(C2H2),whichispurchasedinsteel cylinderscontaining20lbofgasandcosts$10.00exclusiveofthecylinder.Ifawelderis using200ft3perdaymeasuredat16ozgaugeand85°F,whatisthedailycostofacetylene? WhatisthecostperMCFat14.7psiaand60°F? 2.6 (a) A 55,000bbl(nominal)pipelinetankhasadiameterof110ftandaheightof35ft. Itcontains25ftofoilatthetimesuctionistakenontheoilwithpumpsthathandle 20,000bblperday.Thebreatherandsafetyvalveshavebecomecloggedsothatavacuumisdrawnonthetank.Iftheroofisratedtowithstand3/4ozpersqin.pressure,how longwillitbebeforetheroofcollapses?Barometricpressureis29.1in.ofHg.Neglect thefactthattheroofispeakedandthattheremaybesomeleaks. (b) Calculatethetotalforceontheroofatthetimeofcollapse. (c) Ifthetankhadcontainedmoreoil,wouldthecollapsetimehavebeengreaterorless? 2.7 (a) W hatpercentageofmethanebyweightdoesagasof0.65specificgravitycontainifit iscomposedonlyofmethaneandethane?Whatpercentagebyvolume? (b) Explainwhythepercentagebyvolumeisgreaterthanthepercentagebyweight. 2.8 A50-ft3tankcontainsgasat50psiaand50°F.Itisconnectedtoanothertankthatcontains gasat25psiaand50°F.Whenthevalvebetweenthetwoisopened,thepressureequalizes at35psiaat50°F.Whatisthevolumeofthesecondtank? 2.9 Gaswascontractedat$6.00perMCFatcontractconditionsof14.4psiaand80°F.Whatis theequivalentpriceatalegaltemperatureof60°Fandpressureof15.025psia? 2.10 Acylinderisfittedwithaleak-proofpistonandcalibratedsothatthevolumewithinthe cylindercanbereadfromascaleforanypositionofthepiston.Thecylinderisimmersed inaconstanttemperaturebathmaintainedat160°F,whichisthereservoirtemperatureof theSabineGasField.Forty-fivethousandccofthegas,measuredat14.7psiaand60°F,is chargedintothecylinder.Thevolumeisdecreasedinthestepsindicatedasfollows,andthe correspondingpressuresarereadwithadeadweighttesteraftertemperatureequilibriumis reached. V(cc) 2529 964 453 265 180 156.5 142.2 p(psia) 300 750 1500 2500 4000 5000 6000 (a) Calculateandplaceintabularformthegasdeviationfactorsandtheidealvolumesthat theinitial45,000ccoccupiesat160°Fandateachpressure. (b) Calculatethegasvolumefactorsateachpressure,inunitsofft3/SCF. (c) Plotthedeviationfactorandthegasvolumefactorscalculatedinpart(b)versuspressureonthesamegraph. Chapter 2 66 • Review of Rock and Fluid Properties 2.11 (a) I ftheSabineFieldgasgravityis0.65,calculatethedeviationfactorsfromzeroto6000 psiaat160°F,in1000lbincrements,usingthegasgravitycorrelationfromFig.2.2. (b) UsingthecriticalpressuresandtemperaturesinTable2.1,calculateandplotthedeviationfactorsfortheSabinegasatseveralpressuresand160°F.Thegasanalysisisas follows: Component Molefraction Component Molefraction C1 C2 C3 iC4 nC4 iC5 0.875 0.083 0.021 0.006 0.008 0.003 nC5 C6 C7+ 0.002 0.001 0.001 Use the molecular weight and critical temperature and pressure of n-octane for the heptanes-plus.PlotthedataofProblem2.10(a)andProblem2.11(a)onthesamegraph forcomparison. (c) Belowwhatpressureat160°FmaytheidealgaslawbeusedforthegasoftheSabine Fieldiferrorsaretobekeptwithin2%? (d) Will a reservoir contain more SCF of a real or an ideal gas at similar conditions? Explain. 2.12 Ahigh-pressurecellhasavolumeof0.330ft3andcontainsgasat2500psiaand130°F,at which conditions its deviation factor is 0.75.When 43.6 SCF measured at 14.7 psia and 60°Fwerebledfromthecellthroughawettestmeter,thepressuredroppedto1000psia,the temperatureremainingat130°F.Whatisthegasdeviationfactorat1000psiaand130°F? 2.13 Adrygasreservoirisinitiallyatanaveragepressureof6000psiaandtemperatureof160°F. Thegashasaspecificgravityof0.65.Whatwilltheaveragereservoirpressurebewhenonehalfoftheoriginalgas(inSCF)hasbeenproduced?Assumethevolumeoccupiedbythegas inthereservoirremainsconstant.Ifthereservoiroriginallycontained1MMft3ofreservoir gas,howmuchgashasbeenproducedatafinalreservoirpressureof500psia? 2.14 Areservoirgashasthefollowinggasdeviationfactorsat150°F: p(psia) z 0 500 1000 2000 3000 4000 5000 1.00 0.92 0.86 0.80 0.82 0.89 1.00 Plotzversuspandgraphicallydeterminetheslopesat1000psia,2200psia,and4000psia. Then,usingEq.(2.19),findthegascompressibilityatthesepressures. Problems 67 2.15 UsingEqs.(2.9)and(2.10)foranassociatedgasandFig.2.2,findthecompressibilityofa 70%specificgravitygasat5000psiaand203°F. 2.16 UsingEq.(2.21)andthegeneralizedchartforgasdeviationfactors,Fig.2.2,findthepseudoreduced compressibility of a gas at a pseudoreduced temperature of 1.30 and a pseudoreducedpressureof4.00.CheckthisvalueonFig.2.4. 2.17 Estimatetheviscosityofagascondensatefluidat7000psiaand220°F.Ithasaspecific gravityof0.90andcontains2%nitrogen,4%carbondioxide,and6%hydrogensulfide. 2.18 Experimentsweremadeonabottom-holesampleofthereservoirliquidtakenfromthe LaSalleOilFieldtodeterminethesolutiongasandtheformationvolumefactorasfunctions of pressure. The initial bottom-hole pressure of the reservoir was 3600 psia, and the bottom-hole temperature was 160°F; thus all measurements in the laboratory were madeat160°F.Thefollowingdata,convertedtopracticalunits,wereobtainedfromthe measurements: (a) (b) (c) (d) (e) (f) Pressure (psia) Solution gas (SCF/STB) at 14.7 psia and 60°F Formation volume factor (bbl/STB) 3600 567 1.310 3200 567 1.317 2800 567 1.325 2500 567 1.333 2400 554 1.310 1800 436 1.263 1200 337 1.210 600 223 1.140 200 143 1.070 Whichfactorsaffectthesolubilityofgasincrudeoil? Plotthegasinsolutionversuspressure. Wasthereservoirinitiallysaturatedorundersaturated?Explain. Doesthereservoirhaveaninitialgascap? Intheregionof200to2500psia,determinethesolubilityofthegasfromyourgraph inSCF/STB/psi. Suppose1000SCFofgashadaccumulatedwitheachstock-tankbarrelofoilinthis reservoirinsteadof567SCF.Estimatehowmuchgaswouldhavebeeninsolutionat 3600psia.Wouldthereservoiroilthenbecalledsaturatedorundersaturated? Chapter 2 68 • Review of Rock and Fluid Properties 2.19 Fromthebottom-holesamplegiveninProblem2.18, (a) Plottheformationvolumefactorversuspressure. (b) Explainthebreakinthecurve. (c) Whyistheslopeabovethebubble-pointpressurenegativeandsmallerthanthepositive slopebelowthebubble-pointpressure? (d) Ifthereservoircontains250MMreservoirbarrelsofoilinitially,whatistheinitial numberofSTBinplace? (e) Whatistheinitialvolumeofdissolvedgasinthereservoir? (f) Whatwillbetheformationvolumefactoroftheoilwhenthebottom-holepressureisessentiallyatmosphericifthecoefficientofexpansionofthestock-tankoilis0.0006per°F? 2.20 Ifthegravityofthestock-tankoiloftheBigSandyreservoiris30°APIandthegravityof thesolutiongasis0.80°API,estimatethesolutiongas-oilratioandthesingle-phaseformationvolumefactorat2500psiaand165°F.Thesolutiongas-oilratioatthebubble-point pressureof2800psiais625SCF/STB. 2.21 A1000-ft3tankcontains85STBofcrudeoiland20,000SCFofgas,allat120°F.When equilibriumisestablished(i.e.,whenasmuchgashasdissolvedintheoilaswill),thepressureinthetankis500psia.Ifthesolubilityofthegasinthecrudeis0.25SCF/STB/psi andthedeviationfactorforthegasat500psiaand120°Fis0.90,findtheliquidformation volumefactorat500psiaand120°F. 2.22 Acrudeoilhasacompressibilityof20×10–6 psi–1andabubblepointof3200psia.Calculate therelativevolumefactorat4400psia(i.e.,thevolumerelativetoitsvolumeatthebubble point),assumingconstantcompressibility. 2.23 (a) E stimatetheviscosityofanoilat3000psiaand130°F.Ithasastock-tankgravityof 35°APIat60°Fandcontainsanestimated750SCF/STBofsolutiongasattheinitial bubblepointof3000psia. (b) Estimatetheviscosityattheinitialreservoirpressureof4500psia. (c) Estimatetheviscosityat1000psiaifthereisanestimated300SCF/STBofsolution gasatthatpressure. 2.24 Seethefollowinglaboratorydata: Cell pressure (psia) Oil volume in cell (cc) Gas volume in cell (cc) Cell temperature (°F) 2000 650 0 195 1500=Pbp 669 0 195 1000 650 150 195 (continued) References 69 Cell pressure (psia) Oil volume in cell (cc) Gas volume in cell (cc) Cell temperature (°F) 500 615 700 195 14.7 500 44,500 60 EvaluateRso, Bo, and Btatthestatedpressures.Thegasdeviationfactorsat1000psiaand 500psiahavebeenevaluatedas0.91and0.95,respectively. 2.25 (a) F indthecompressibilityforaconnatewaterthatcontains20,000partspermillionof totalsolidsatareservoirpressureof4000psiaandtemperatureof150°F. (b) Findtheformationvolumefactoroftheformationwaterofpart(a). 2.26 (a) W hatistheapproximateviscosityofpurewateratroomtemperatureandatmospheric pressure? (b) Whatistheapproximateviscosityofpurewaterat200°F? 2.27 Acontainerhasavolumeof500ccandisfullofpurewaterat180°Fand6000psia. (a) Howmuchwaterwouldbeexpelledifthepressurewasreducedto1000psia? (b) Whatwouldbethevolumeofwaterexpelledifthesalinitywas20,000ppmandthere wasnogasinsolution? (c) Reworkpart(b)assumingthatthewaterisinitiallysaturatedwithgasandthatallthe gasisevolvedduringthepressurechange. (d) Estimatetheviscosityofthewater. References 1. R.P.Monicard,Properties of Reservoir Rocks: Core Analysis,GulfPublishingCo.,1980. 2. B.J.Dotson,R.L.Slobod,P.N.McCreery,andJamesW.Spurlock,“Porosity-Measurement ComparisonsbyFiveLaboratories,”Trans.AlME(1951),192,344. 3. N.Ezekwe,Petroleum Reservoir Engineering Practice,PearsonEducation,2011. 4. W. van der Knaap, “Non-linear Elastic Behavior of Porous Media,” presented before the SocietyofPetroleumEngineersofAlME,Oct.1958,Houston,TX. 5. G.H.Newman,“Pore-VolumeCompressibilityofConsolidated,Friable,andUnconsolidatedReservoirRocksunderHydrostaticLoading,”Jour. of Petroleum Technology(Feb.1973), 129–34. 6. J.Geertsma,“TheEffectofFluidPressureDeclineonVolumetricChangesofPorousRocks,” Jour. of Petroleum Technology(1957),11,No.12,332. 7. HenryJ.GruyandJackA.Crichton,“ACriticalReviewofMethodsUsedintheEstimationof NaturalGasReserves,”Trans.AlME(1949),179,249–63. 70 Chapter 2 • Review of Rock and Fluid Properties 8. R.P.Sutton,“FundamentalPVTCalculationsforAssociatedandGas/CondensateNatural-Gas Systems,”SPE Res. Eval. & Eng.(2007),10,No.3,270–84. 9. MarshallB.StandingandDonaldL.Katz,“DensityofNaturalGases,”Trans.AlME(1942), 146,144. 10. P.M.DranchukandJ.H.Abou-Kassem,“CalculationofZFactorsforNaturalGasesUsing EquationsofState,”Jour. of Canadian Petroleum Technology(July–Sept.1975),14,No.3, 34–36. 11. R.W.Hornbeck,Numerical Methods,QuantumPublishers,1975. 12. C.KennethEilertsetal.,Phase Relations of Gas-Condensate Fluids,Vol.10,USBureauof MinesMonograph10,AmericanGasAssociation,1957,427–34. 13. E.WichertandK.Aziz,“CalculateZ’sforSourGases,”Hyd. Proc.(May1972),119–22. 14. A.S.Trube,“CompressibilityofNaturalGases,”Trans.AlME(1957),210,61. 15. L. Mattar, G. S. Brar, and K.Aziz, “Compressibility of Natural Gases,” JCPT (Oct.–Dec. 1975),77–80. 16. T.A. Blasingame, J. L. Johnston, and R. D. Poe Jr., Properties of Reservoir Fluids,Texas A&MUniversity,1989. 17. N.L.Carr,R.Kobayashi,andD.B.Burrows,“ViscosityofHydrocarbonGasesunderPressure,”Trans.AlME(1954),201,264–72. 18. A.L.Lee,M.H.Gonzalez,andB.E.Eakin,“TheViscosityofNaturalGases,”Jour. of Petroleum Technology(Aug.1966),997–1000;Trans.AlME(1966),237. 19. W.D.McCain,J.P.Spivey,andC.P.Lenn,Petroleum Reservoir Fluid Property Correlations, PennWellPublishing,2011. 20. P.P.ValkoandW.D.McCain,“ReservoirOilBubble-PointPressuresRevisited:SolutionGasOilRatiosandSurfaceGasSpecificGravities,”Jour. of Petroleum Science and Engineering (2003),37,153–69. 21. J.J.Velarde,T.A.Blasingame,andW.D.McCain,“CorrelationofBlackOilPropertiesat PressuresbelowBubblePointPressure—ANewApproach,”CIM 50-Year Commemorative Volume, CanadianInstituteofMining,1999. 22. J.P.Spivey,P.P.Valko,andW.D.McCain,“ApplicationsoftheCoefficientofIsothermal CompressibilitytoVariousReservoirSituationswithNewCorrelationsforEachSituation,” SPE Res. Eval. & Eng.(2007),10,No.1,43–49. 23. A.J.Villena-Lanzi,“ACorrelationfortheCoefficientofIsothermalCompressibilityofBlack OilatPressuresbelowtheBubblePoint,”master’sthesis,TexasA&MUniversity,1985,CollegeStation,TX. 24. E. O. Egbogah, “An Improved Temperature-Viscosity Correlation for Crude Oil Systems,” paper83-34-32,presentedatthe1983AnnualTechnicalMeetingofthePetroleumSocietyof CIM,May10–13,1983,Alberta,Canada. References 71 25. H.D.Beggs,“OilSystemCorrelations,”Petroleum Engineering Handbook,ed.H.C.Bradley, SocietyofPetroleumEngineers,1987. 26. H.D.BeggsandJ.R.Robinson,“EstimatingtheViscosityofCrudeOilSystems,”Jour. of Petroleum Technology(Sept.1975),1140–41. 27. G. E. Petrosky and F. F. Farshad, “Viscosity Correlations for Gulf of Mexico Crude Oils,” paperSPE29468,presentedattheSPEProductionOperationsSymposium,1995,Oklahoma City. 28. W. D. McCain Jr., “Reservoir-Fluid Property Correlations: State of theArt,” SPERE (May 1991),266. 29. T. L. Osif, “The Effects of Salt, Gas,Temperature, and Pressure on the Compressibility of Water,”SPERE(Feb.1988),175–81. This page intentionally left blank C H A P T E R 3 The General Material Balance Equation 3.1 Introduction Fluiddoesnotleaveavoidspacebehind,asitisproducedfromahydrocarbonreservoir.Asthe pressureinthereservoirdropsduringtheproductionoffluids,theremainingfluidsand/orreservoirrockexpandornearbywaterencroachestofillthespacecreatedbyanyproducedfluids.The volumeofoilproducedonthesurfaceaidsthereservoirengineerindeterminingtheamountofthe expansionorencroachmentthatoccursinthereservoir.Materialbalanceisamethodthatcanbe usedtoaccountforthemovementofreservoirfluidswithinthereservoirortothesurfacewhere theyareproduced.Thematerialbalanceaccountsforthefluidproducedfromthereservoirthrough expansionofexistingfluid,expansionoftherock,orthemigrationofwaterintothereservoir.A general material balance equation that can be applied to all reservoir types is developed in this chapter.Thematerialbalanceequationincludesfactorsthatcomparethevariouscompressibilities offluids,considerthegassaturatedintheliquidphase,andincludethewaterthatmayenterintothe hydrocarbonreservoirfromaconnectedaquifer.Fromthisgeneralequation,eachoftheindividual equationsforthereservoirtypesdefinedinChapter1anddiscussedinsubsequentchapterscan easilybederivedbyconsideringtheimpactofthevarioustermsofthematerialbalanceequation. ThegeneralmaterialbalanceequationwasfirstdevelopedbySchilthuisin1936.1Sincethat time,theuseofcomputersandsophisticatedmultidimensionalmathematicalmodelshavereplaced thezero-dimensionalSchilthuisequationinmanyapplications.2However,theSchilthuisequation, iffullyunderstood,canprovidegreatinsightforthepracticingreservoirengineer.Followingthe derivationofthegeneralmaterialbalanceequation,amethodofusingtheequationdiscussedinthe literaturebyHavlenaandOdehispresented.3,4 3.2 Derivation of the Material Balance Equation Whenanoilandgasreservoiristappedwithwells,oilandgas,andfrequentlysomewater,areproduced,therebyreducingthereservoirpressureandcausingtheremainingoilandgastoexpandto fillthespacevacatedbythefluidsremoved.Whentheoil-andgas-bearingstrataarehydraulically 73 Chapter 3 74 • The General Material Balance Equation connectedwithwater-bearingstrata(aquifers)withbulkvolumemuchgreaterthanthatofthehydrocarbonzone,waterencroachesintothereservoirasthepressuredropsowingtoproduction,as illustratedinFig.3.1.Thiswaterencroachmentdecreasestheextenttowhichtheremainingoiland gasexpandandaccordinglyretardsthedeclineinreservoirpressure.Inasmuchasthetemperature inoilandgasreservoirsremainssubstantiallyconstantduringthecourseofproduction,thedegree towhichtheremainingoilandgasexpanddependsonthepressureandthecompositionoftheoil andgas.Bytakingbottom-holesamplesofthereservoirfluidsunderpressureandmeasuringtheir relativevolumesinthelaboratoryatreservoirtemperatureandundervariouspressures,itispossibletopredicthowthesefluidsbehaveinthereservoirasreservoirpressuredeclines. InChapter6,itisshownthat,althoughtheconnatewaterandformationcompressibilities are quite small, they are, relative to the compressibility of reservoir fluids above their bubble points,significant,andtheyaccountforanappreciablefractionoftheproductionabovethebubblepoint.Table3.1givesarangeofvaluesforformationandfluidcompressibilitiesfromwhich itmaybeconcludedthatwaterandformationcompressibilitiesarelesssignificantingasandgas Oil, gas-cap gas, and solution gas Oil and solution gas Oil, solution gas, and water Gas cap Original gas-oil contact Gas-cap expansion Gas saturation building up in oil zone caused by gas coming out of solution in oil Oil zone Water influx Original oil-water contact Aquifier Figure 3.1 Cross section of a combination drive reservoir (after Woody and Moscrip, trans. AlME).5 3.2 Derivation of the Material Balance Equation 75 Table 3.1 Range of Compressibilities Formationrock 3–10×10–6 psi–1 Water 2–4×10–6 psi–1 Undersaturatedoil 5–100×10–6 psi–1 Gasat1000psi 900–1300×10–6 psi–1 Gasat5000psi 50–200×10–6 psi–1 capreservoirsandinundersaturatedreservoirsbelowthebubblepointwherethereisappreciablegassaturation.Becauseofthisandthecomplicationstheywouldintroduceinalreadyfairly complex equations, water and formation compressibilities are generally neglected, except in undersaturatedreservoirsproducingabovethebubblepoint.Atermaccountingforthechangein waterandformationvolumesowingtotheircompressibilitiesisincludedinthematerialbalance derivation,andtheengineercanchoosetoeliminatethisforparticularapplications.Thegasin solutionintheformationwaterisneglected,andinmanyinstances,thevolumeoftheproduced waterisnotknownwithsufficientaccuracytojustifytheuseofaformationvolumefactorwith theproducedwater. Thegeneralmaterialbalanceequationissimplyavolumetricbalance,whichstatesthatsince thevolumeofareservoir(asdefinedbyitsinitiallimits)isaconstant,thealgebraicsumofthe volumechangesoftheoil,freegas,water,androckvolumesinthereservoirmustbezero.For example,ifboththeoilandgasreservoirvolumesdecrease,thesumofthesetwodecreasesmust bebalancedbychangesofequalmagnitudeinthewaterandrockvolumes.Iftheassumptionis madethatcompleteequilibriumisattainedatalltimesinthereservoirbetweentheoilanditssolutiongas,itispossibletowriteageneralizedmaterialbalanceexpressionrelatingthequantitiesof oil,gas,andwaterproduced;theaveragereservoirpressure;thequantityofwaterthatmayhave encroachedfromtheaquifer;andfinallytheinitialoilandgascontentofthereservoir.Inmaking thesecalculations,thefollowingproduction,reservoir,andlaboratorydataareinvolved: 1. Theinitialreservoirpressureandtheaveragereservoirpressureatsuccessiveintervalsafter thestartofproduction. 2. Thestock-tankbarrelsofoilproduced,measuredat1atmand60°F,atanytimeorduringany productioninterval. 3. Thetotalstandardcubicfeetofgasproduced.Whengasisinjectedintothereservoir,this willbethedifferencebetweenthetotalgasproducedandthatreturnedtothereservoir. 4. Theratiooftheinitialgascapvolumeandtheinitialoilvolume,m: m= Initialreservoir freegasvolume Initialreserrvoir oilvolume Chapter 3 76 • The General Material Balance Equation If the value of m can be determined with reasonable precision, there is only one unknown(N)inthematerialbalanceonvolumetricgascapreservoirsandtwo(N and We)in water-drivereservoirs.Thevalueofmisdeterminedfromlogandcoredataandfromwell completion data, which frequently helps to locate the gas-oil and water-oil contacts. The ratiomisknowninmanyinstancesmuchmoreaccuratelythantheabsolutevaluesofthegas capandoilzonevolumes.Forexample,whentherockinthegascapandthatintheoilzone appeartobeessentiallythesame,itmaybetakenastheratioofthenetoreventhegross volumes(withoutknowingtheaverageconnatewateroraverageporosity). 5. Thegasandoilformationvolumefactorsandthesolutiongas-oilratios.Theseareobtained asfunctionsofpressurebylaboratorymeasurementsonbottom-holesamplesbythedifferentialandflashliberationmethods. 6. Thequantityofwaterthathasbeenproduced. 7. Thequantityofwaterthathasbeenencroachedintothereservoirfromtheaquifer. Forsimplicity,thederivationisdividedintothechangesintheoil,gas,water,androckvolumesthatoccurbetweenthestartofproductionandanytimet.Thechangeintherockvolumeis expressedasachangeintheporevolume,whichissimplythenegativeofthechangeintherock volume.Inthedevelopmentofthegeneralmaterialbalanceequation,thefollowingtermsareused: N Boi Np Bo G Bgi Gf Rsoi Rp Rso Bg W Wp Bw We c Δp Swi Vf cf Initialreservoiroil,STB Initialoilformationvolumefactor,bbl/STB Cumulativeproducedoil,STB Oilformationvolumefactor,bbl/STB Initialreservoirgas,SCF Initialgasformationvolumefactor,bbl/SCF Amountoffreegasinthereservoir,SCF Initialsolutiongas-oilratio,SCF/STB Cumulativeproducedgas-oilratio,SCF/STB Solutiongas-oilratio,SCF/STB Gasformationvolumefactor,bbl/SCF Initialreservoirwater,bbl Cumulativeproducedwater,STB Waterformationvolumefactor,bbl/STB Waterinfluxintoreservoir,bbl Totalisothermalcompressibility,psi–1 Changeinaveragereservoirpressure,psia Initialwatersaturation Initialporevolume,bbl Formationisothermalcompressibility,psi–1 Thefollowingexpressiondeterminesthechangeintheoilvolume: 3.2 Derivation of the Material Balance Equation Initialreservoiroilvolume=NBoi Oilvolumeattimetandpressurep=(N – Np)Bo Changeinoilvolume=NBoi –(N – Np)Bo 77 (3.1) Thefollowingexpressiondeterminesthechangeinfreegasvolume: GBgi Ratioofinitialfree gas toinitialoilvolume = m = NB oi Wheninitialfreegasvolume=GBgi = NmBoi, SCFfree SCFinitialgas, SCFgas SCFremaining gas at t = free and dissolved − produced − insolution NmBoi Gf = + NRsoi − [ N p Rp ] − [( N − N p ) Rso ] Bgi Reservoir free gas NmBoi + NRsoi − N p Rp − ( N − N p ) Rso Bg volumeattime t = B gi NmBoi Changeinfree + NRsoi − N p Rp − ( N − N p ) Rso Bg gas volume = NmBoi − B gi (3.2) Thefollowingexpressiondeterminesthechangeinthewatervolume: Initialreservoirwatervolume=W Cumulativewaterproducedatt = Wp Reservoirvolumeofcumulativeproducedwater=Bw Wp Volumeofwaterencroachedatt = We Changein watervolume = W–(W + We – BwWp + Wcw Δp )=–We + BwWp + Wcw Δp (3.3) Chapter 3 78 • The General Material Balance Equation Thefollowingexpressiondeterminesthechangeinthevoidspacevolume: Initialvoidspacevolume=Vf Changeinvoid spacevolume = Vf – [Vf – Vfcf Δp ] = Vfcf Δp Or,becausethechangeinvoidspacevolumeisthenegativeofthechangeinrockvolume, Changein = – V c f f Δp rockvolume (3.4) Combiningthechangesinwaterandrockvolumesintoasingletermyieldsthefollowing: = –We + BwWp – Wcw Δp – Vfcf Δp RecognizingthatW = VfSwi and V f = NBoi + NmBoi andsubstituting,thefollowingisobtained: 1 + Swi NB + NmBoi = –We + BwWp – oi (cw Swi + cf) Δp 1 + Swi or cw Swi + c f = –We + BwWp –(1+m)NBoi Δp 1 − Swi (3.5) Equatingthechangesintheoilandfreegasvolumestothenegativeofthechangesinthewaterand rockvolumesandexpandingalltermsproduces NmBoi Bg N Boi – N Bo + NpBo + NmBoi – – NRsoiBg + NpRpBg Bgi cw Swi + c f + NBgRso – NpBgRso = We – BwWp +(1 + m)NBoi Δp 1 − Swi AddingandsubtractingthetermNpBgRsoiproduces 3.2 Derivation of the Material Balance Equation 79 NmBoi Bg N Boi – N Bo + NpBo + NmBoi – – NRsoiBg + NpRpBg + NBgRso Bgi cw Swi + c f – NpBgRso+ NpBgRsoi – NpBgRsoi = We – BwWp +(1 + m)NBoi Δp 1 − Swi Then,groupingtermsproduces NBoi – NmBoi – N[Bo +(Rsoi – Rso)Bg] + Np[Bo + (Rsoi – Rso)Bg] NmBoi Bg cw Swi + c f +(Rp – Rsoi)BgNp – = We – BwWp +(1 + m)NBoi Δp Bgi 1 − Swi WritingBoi = Bti and [Bo+(Rsoi – Rso)Bg] = Bt,whereBtisthetwo-phaseformationvolumefactor, asdefinedbyEq.(2.29),produces Bg N(Bti – Bt) + Np[Bt + (Rp – Roi)Bg] + NmBti 1 − B gi cw Swi + c f = We – BwWp + (1+ m)NBti Δp 1 − Swi (3.6) Thisisthegeneralvolumetricmaterialbalanceequation.Itcanberearrangedintothefollowing form,whichisusefulfordiscussionpurposes: N(Bt – Bti) + cw Swi + c f NmBti ( Bg − Bgi ) + (1+ m) N Bti Δp + We Bgi 1 − Swi = Np[Bt + (Rp – Rsoi)Bg] + BwWp (3.7) Eachtermontheleft-handsideofEq.(3.7)accountsforamethodoffluidproduction,andeach termontheright-handsiderepresentsanamountofhydrocarbonorwaterproduction.Forillustration purposes,Eq.(3.7)canbewrittenasfollows,witheachmathematicaltermreplacedbyapseudoterm: Oilexpansion+Gasexpansion+Formationandwaterexpansion +Waterinflux=Oilandgasproduction+Waterproduction (3.7a) Theleft-handsideaccountsforallthemethodsofexpansionorinfluxinthereservoirthat woulddrivetheproductionofoil,gas,andwater,thetermsontheright-handside.Oilexpansion 80 Chapter 3 • The General Material Balance Equation isderivedfromtheproductoftheinitialoilinplaceandthechangeinthetwo-phaseoilformation volumefactor.Gasexpansionissimilar;however,additionaltermsareneededtoconverttheinitial oilinplacetoinitialgasinplace—bothfreegasanddissolvedgas.Thethirdtermcanbebroken downintothreepieces.Itistheproductoftheinitialoilandgasinplace,theexpansionofthe connatewaterandtheformationrock,andthechangeinthevolumetricaveragereservoirpressure. Thesethreepiecesaccountfortheexpansionoftheconnatewaterandtheformationrockinthe reservoir. Ontheright-handside,theoilandgasproducedisdeterminedbyconsideringthevolumeoftheproducedoilifitwereinthereservoir.Theproducedoilismultipliedbythesum of the two-phase oil formation volume factor and the volume factor of gas liberated as the pressurehasdeclined.Theproducedwaterissimplytheproductoftheproducedwaterandits volumefactor. Equation(3.7)canbearrangedtoapplytoanyofthedifferentreservoirtypesdiscussedin Chapter1.Withouteliminatinganyterms,Eq.(3.7)isusedforthecaseofasaturatedoilreservoirwithanassociatedgascap.ThesereservoirsarediscussedinChapter7.Whenthereisno originalfreegas,suchasinanundersaturatedoilreservoir(discussedinChapter6),m=0,and Eq.(3.7)reducesto cw Swi + c f N(Bt – Bti) + NBti Δp + We = Np[Bt + (Rp – Rsoi)Bg] + BwWp 1 − Swi (3.8) Forgasreservoirs,Eq.(3.7)canbemodifiedbyrecognizingthatNPRP = Gp and NmBti = GBgi and substitutingthesetermsintoEq.(3.7): c S +cf N(Bt – Bti) +G (Bg – Bgi)+ (NBti + GBgi) w wi 1 − Swi Δp + We = NpBt + (Gp – NRsoi)Bg + BwWp (3.9) Whenworkingwithgasreservoirs,thereisnoinitialoilamount;therefore,N and Npequalzero. Thegeneralmaterialbalanceequationforagasreservoircanthenbeobtained: c S +cf G (Bg – Bgi)+GBgi w wi Δp + We = Gp Bg+ BwWp 1 − Swi (3.10) Thisequationisdiscussedinconjunctionwithgasandgas-condensatereservoirsinChapters4and5. Inthestudyofreservoirsthatareproducedsimultaneouslybythethreemajormechanisms ofdepletiondrive,gascapdrive,andwaterdrive,itisofpracticalinteresttodeterminetherelativemagnitudeofeachofthesemechanismsthatcontributetotheproduction.Pirsonrearranged thematerialbalanceEq.(3.7)asfollowstoobtainthreefractions,whosesumisone,whichhe calledthedepletiondriveindex(DDI),thesegregation(gascap)driveindex(SDI),andthewater-driveindex(WDI).6 3.3 Uses and Limitations of the Material Balance Method 81 Whenallthreedrivemechanismsarecontributingtotheproductionofoilandgasfromthe reservoir,thecompressibilityterminEq.(3.7)isnegligibleandcanbeignored.Movingthewater productiontermtotheleft-handsideoftheequation,thefollowingisobtained: N(Bt – Bti) + NmBti (Bg – Bgi) + (We – BwWp) = Np[Bt + (Rp – Rsoi)Bg] Bgi Dividingthroughbythetermontheright-handsideoftheequationproduces NmBti ( Bg − Bgi ) Bgi N ( Bt − Bti ) + N p [ Bt + ( Rp − Rsoi ) Bg ] N p [ Bt + ( R p − Rsoi ) Bg ] + (We − BwW p ) N p [ Bt + ( Rp − Rsoi ) Bg ] =1 (3.11) Thenumeratorsofthethreefractionsthatappearontheleft-handsideofEq.(3.11)aretheexpansionoftheinitialoilzone,theexpansionoftheinitialgaszone,andthenetwaterinflux,respectively.Thecommondenominatoristhereservoirvolumeofthecumulativegasandoilproduction expressedatthelowerpressure,whichevidentlyequalsthesumofthegasandoilzoneexpansions plusthenetwaterinflux.Then,usingPirson’sabbreviations, DDI+SDI+WDI=1 calculationsareperformedinChapter7toillustratehowthesedriveindicescanbeused. 3.3 Uses and Limitations of the Material Balance Method Thematerialbalanceequationderivedintheprevioussectionhasbeeningeneraluseformany years,mainlyforthefollowing: 1. Determiningtheinitialhydrocarboninplace 2. Calculatingwaterinflux 3. Predictingreservoirpressures Althoughinsomecasesitispossibletosolvesimultaneouslytofindtheinitialhydrocarbonandthe waterinflux,generallyoneortheothermustbeknownfromdataormethodsthatdonotdepend onthematerialbalancecalculations.Oneofthemostimportantusesoftheequationsispredicting theeffectofcumulativeproductionand/orinjection(gasorwater)onreservoirpressure;therefore, 82 Chapter 3 • The General Material Balance Equation itisverydesirabletoknowinadvancetheinitialoilandtheratiomfromgoodcoreandlogdata. Thepresenceofanaquiferisusuallyindicatedbygeologicevidence;however,thematerialbalance maybeusedtodetecttheexistenceofawaterdrivebycalculatingthevalueoftheinitialhydrocarbonatsuccessiveproductionperiods,assumingzerowaterinflux.Unlessothercomplicating factors are present, the constancy in the calculated value of N and/or G indicates a volumetric reservoir,andcontinuallychangingvaluesofN and Gindicateawaterdrive. Theprecisionofthecalculatedvaluesdependsontheaccuracyofthedataavailabletosubstituteintheequationandontheseveralassumptionsthatunderlietheequations.Onesuchassumption istheattainmentofthermodynamicequilibriuminthereservoir,mainlybetweentheoilanditssolutiongas.WielandandKennedyhavefoundatendencyfortheliquidphasetoremainsupersaturated withgasasthepressuredeclines.7Saturationpressurediscrepanciesbetweenfluidandcoremeasurementsandmaterialbalanceevidenceintherangeof19psifortheEastTexasFieldand25psifor theSlaughterFieldwereobserved.Theeffectofsupersaturationcausesreservoirpressureforagiven volumeofproductiontobelowerthanitotherwisewouldhavebeen,hadequilibriumbeenattained. ItisalsoimplicitlyassumedthatthePVTdatausedinthematerialbalanceanalysesareobtained usinggasliberationprocessesthatcloselyduplicatethegasliberationprocessesinthereservoir,inthe well,andinseparatorsonthesurface.ThismatterisdiscussedindetailinChapter7,anditisonlystated herethatPVTdatabasedongasliberationprocessesthatvarywidelyfromtheactualreservoirdevelopmentcancauseconsiderableerrorinthematerialbalanceresultsandimplications. Anothersourceoferrorisintroducedinthedeterminationofaveragereservoirpressure at the end of any production interval.Aside from instrument errors and those introduced by difficultiesinobtainingtruestaticorfinalbuilduppressures(seeChapter8),thereisoftenthe problemofcorrectlyweightingoraveragingtheindividualwellpressures.Forthickerformationswithhigherpermeabilitiesandoilsoflowerviscosities,wherefinalbuilduppressuresare readilyandaccuratelyobtainedandwhenthereareonlysmallpressuredifferencesacrossthe reservoir,reliablevaluesofaveragereservoirpressureareeasilyobtained.Ontheotherhand, forthinnerformationsoflowerpermeabilityandoilsofhigherviscosity,difficultiesaremetin obtainingaccuratefinalbuilduppressures,andthereareoftenlargepressurevariationsthroughoutthereservoir.Thesearecommonlyaveragedbypreparingisobaricmapssuperimposedon isopachmaps.Thismethodusuallyprovidesreliableresultsunlessthemeasuredwellpressures areerraticandthereforecannotbeaccuratelycontoured.Thesedifferencesmaybeduetovariationsinformationthicknessandpermeabilityandinwellproductionandproducingrates.Also, difficultiesareencounteredwhenproductionfromtwoormoreverticallyisolatedzonesorstrata ofdifferentproductivityarecommingled.Inthiscase,thepressuresaregenerallyhigherinthe strataoflowproductivity,andbecausethemeasuredpressuresarenearertothoseinthezones ofhighproductivity,themeasuredstaticpressurestendtobelowerandthereservoirbehavesas ifitcontainedlessoil.Schilthuisexplainedthisphenomenonbyreferringtotheoilinthemore productivezonesasactiveoilandbyobservingthatthecalculatedactiveoilusuallyincreases withtimebecausetheoilandgasinthezonesoflowerproductivityslowlyexpandtohelpoffset thepressuredecline.Uncertaintiesassociatedwithassessingproductionfromcommingledreservoirzonesmotivateregulatoryrestrictionsforthisreservoirmanagementstrategy.Fieldsthatare 3.4 The Havlena and Odeh Method of Applying the Material Balance Equation 83 notfullydevelopedmayalsoshowsimilarapparentincreaseinactiveoilproductionbecausethe apparentaveragepressurecanbethatofthedevelopedportiononlywhilethepressureisactually higherintheundevelopedportions. Theeffectofpressureerrorsoncalculatedvaluesofinitialoilorwaterinfluxdependsonthe sizeoftheerrorsinrelationtothereservoirpressuredecline.Thisistruebecausepressureenters thematerialbalanceequationmainlyasdifferences(Bo – Boi),(Rsi – Rs),and(Bg – Bgi).Because waterinfluxandgascapexpansiontendtooffsetpressuredecline,thepressureerrorsaremore seriousthanfortheundersaturateddepletionreservoirs.Inthecaseofveryactivewaterdrivesand gascapsthatarelargecomparedwiththeassociatedoilzone,thematerialbalanceisuselesstodeterminetheinitialoilinplacebecauseoftheverysmallpressuredecline.Hutchinsonemphasized theimportanceofobtainingaccuratevaluesofstaticwellpressuresinhisquantitativestudyofthe effectofdataerrorsonthevaluesofinitialgasorofinitialoilinvolumetricgasorundersaturated oilreservoirs,respectively.8 Uncertaintiesintheratiooftheinitialfreegasvolumetotheinitialreservoiroilvolume also affect the calculations. The error introduced in the calculated values of initial oil, water influx, or pressure increases with the size of this ratio because, as explained in the previous paragraph,largergascapsreducetheeffectofpressuredecline.Forquitelargegascapsrelative totheoilzone,thematerialbalanceapproachesagasbalancemodifiedslightlybyproduction fromtheoilzone.Thevalueofmisobtainedfromcoreandlogdatausedtodeterminethenet productivebulkgasandoilvolumesandtheiraverageporositiesandinterstitialwater.Because thereisfrequentlyoilsaturationinthegascap,theoilzonemustincludethisoil,whichcorrespondinglydiminishestheinitialfreegasvolume.Welltestsareoftenusefulinlocatinggas-oil andwater-oilcontactsinthedeterminationofm.Insomecases,thesecontactsarenothorizontal planesbutaretilted,owingtowatermovementintheaquifer,ordishshaped,owingtotheeffect ofcapillarityinthelesspermeableboundaryrocksofvolumetricreservoirs. Whereasthecumulativeoilproductionisgenerallyknownquiteprecisely,thecorresponding gasandwaterproductionisusuallymuchlessaccurateandthereforeintroducesadditionalsources oferrors.Thisisparticularlytruewhenthegasandwaterproductionisnotdirectlymeasuredbut mustbeinferredfromperiodicteststodeterminethegas-oilratiosandwatercutsoftheindividual wells.Whentwoormorewellscompletedindifferentreservoirsareproducingtocommonstorage, unlessthereareindividualmetersonthewells,onlytheaggregateproductionisknownandnotthe individualoilproductionfromeachreservoir.Underthecircumstancesthatexistinmanyfields,it isdoubtfulthatthecumulativegasandwaterproductionisknowntowithin10%,andinsomeinstances,theerrorsmaybelarger.Withthegrowingimportanceofnaturalgasandbecausemoreof thegasassociatedwiththeoilisbeingsold,bettervaluesofgasproductionarebecomingavailable. 3.4 The Havlena and Odeh Method of Applying the Material Balance Equation Asearlyas1953,vanEverdingen,Timmerman,andMcMahonrecognizedamethodofapplying thematerialbalanceequationasastraightline.9Butitwasn’tuntilHavlenaandOdehpublished 84 Chapter 3 • The General Material Balance Equation their work that the method became fully exploited.3,4 Normally, when using the material balance equation, an engineer considers each pressure and the corresponding production data as beingseparatepointsfromotherpressurevalues.Fromeachseparatepoint,acalculationfora dependentvariableismade.Theresultsofthecalculationsaresometimesaveraged.TheHavlena-Odehmethodusesallthedatapoints,withthefurtherrequirementthatthesepointsmust yieldsolutionstothematerialbalanceequationthatbehavelinearlytoobtainvaluesoftheindependentvariable. Thestraight-linemethodbeginswiththematerialbalanceequationwrittenas Np[Bt + (Rp – Rsoi)Bg] + BwWp – WI – GIBIg cw Swi + c f = N ( Bt − Bti ) + Bti (1 + m ) 1 + Swi mBti Δp + B ( Bg − Bgi ) + We gi (3.12) ThetermsWI(cumulativewaterinjection),GI(cumulativegasinjection),andBIg(formationvolumefactoroftheinjectedgas)havebeenaddedtoEq.(3.7).InHavlenaandOdeh’soriginaldevelopment,theychosetoneglecttheeffectofthecompressibilitiesoftheformationandconnate waterinthegascapportionofthereservoir—thatis,intheirdevelopment,thecompressibilityterm ismultipliedbyNandnotbyN(1+m).InEq.(3.12),thecompressibilitytermismultipliedby N(1+m)forcompleteness.Youmaychoosetoignorethe(1+m)multiplierinparticularapplications.HavlenaandOdehdefinedthefollowingtermsandrewroteEq.(3.12)as F = Np[Bt + (Rp – Rsoi)Bg] + BwWp –WI – GIBIg Eo= Bt – Bti cw Swi + c f E f,w = ΔP 1 − Swi Eg = Bg – Bgi NmBti F = NEo + N(1 + m)Bti Ef, w + Eg +We Bgi (3.13) In Eq. (3.13), F represents the net production from the reservoir. Eo, Ef,w, and Eg represent the expansionofoil,formationandwater,andgas,respectively.HavlenaandOdehexaminedseveral casesofvaryingreservoirtypeswiththisequationandfoundthattheequationcanberearranged intotheformofastraightline.Forinstance,considerthecaseofnooriginalgascap,nowater influx,andnegligibleformationandwatercompressibilities.Withtheseassumptions,Eq.(3.13) References 85 reducesto F = NEo (3.14) ThiswouldsuggestthataplotofFastheycoordinateandEoasthexcoordinatewouldyielda straightlinewithslopeNandinterceptequaltozero.Additionalcasescanbederived,asshownin Chapter7. Oncealinearrelationshiphasbeenobtained,theplotcanbeusedasapredictivetoolforestimatingfutureproduction.Examplesareshowninsubsequentchapterstoillustratetheapplication oftheHavlena-Odehmethod. References 1. RalphJ.Schilthuis,“ActiveOilandReservoirEnergy,”Trans.AlME(1936),118,33. 2. L.P.Dake,Fundamentals of Reservoir Engineering,Elsevier,1978,73–102. 3. D.HavlenaandA.S.Odeh,“TheMaterialBalanceasanEquationofaStraightLine:PartI,” Jour. of Petroleum Technology(Aug.1963),896–900. 4. D.HavlenaandA.S.Odeh,“TheMaterialBalanceasanEquationofaStraightLine:Part II—FieldCases,”Jour. of Petroleum Technology(July1964),815–22. 5. L.D.WoodyJr.andRobertMoscripIII,“PerformanceCalculationsforCombinationDrive Reservoirs,”Trans.AlME(1956),207,129. 6. SylvainJ.Pirson,Elements of Oil Reservoir Engineering,2nded.,McGraw-Hill,1958,635–93. 7. DentonR.WielandandHarveyT.Kennedy,“MeasurementsofBubbleFrequencyinCores,” Trans.AlME(1957),210,125. 8. CharlesA.Hutchinson,“EffectofDataErrorsonTypicalEngineeringCalculations,”presentedattheOklahomaCitymeetingoftheAlMEpetroleumbranch,1951. 9. A.F.vanEverdingen,E.H.Timmerman,andJ.J.McMahon,“ApplicationoftheMaterial BalanceEquationtoaPartialWater-DriveReservoir,”Trans.AlME(1953),198,51. This page intentionally left blank C H A P T E R 4 Single-Phase Gas Reservoirs 4.1 Introduction Thischaptercontainsadiscussionofsingle-phasegasreservoirs(refertoFig.1.4).Inasingle-phase gasreservoir,thereservoirfluid,usuallycallednaturalgas,remainsasnonassociatedgasduring theentireproducinglifeofthereservoir.Thistypeofreservoirisfrequentlyreferredtoasadrygas reservoirbecausenocondensateisformedinthereservoirduringthelifeofproduction.However, manyofthesewellsdoproducecondensate,becausethetemperatureandpressureconditionsin theproducingwellandatthesurfacecanbesignificantlydifferentfromthereservoirtemperature andpressure.Thischangeinconditionscancausesomecomponentsintheproducinggasphase tocondenseandbeproducedasliquid.Theamountofcondensationisafunctionofnotonlythe pressureandtemperaturebutalsothecompositionofthenaturalgas,whichtypicallyconsistsprimarilyofmethaneandethane.Thetendencyforcondensatetoformonthesurfaceincreasesasthe concentrationofheaviercomponentsincreasesinthereservoirfluid. Inbeginninganytypeofreservoiranalysis,specificinformationaboutthereservoirmustbe obtainedinordertoestimatethetotalhydrocarboninplaceinthereservoir.Asthischapterfocuses exclusivelyongas,thisanalysiswillbepresentedbywayofcalculatingatotalgasinplace.Typically,thereservoirformationwillbemappedbyseismicdatathatwillallowforthedetermination ofthearealextentofthereservoir(thetotalacreageoftheundergroundformation)andalsothe reservoirthickness.Thesevaluesarethenmultipliedtogethertodeterminetheinitialbulkvolume ofthereservoir.Coresamplestakenfromappraisalwellswillestablishporosityandtherelative fractionsofoil,gas,andwater.ThesearetypicallydenotedSoforoil,Sgforgas,andSwforwater. Theletteri,whenaddedtothesubscript,denotestheinitialvalueofthatfraction. Asecondcrucialpieceofinformationtobedeterminedbeforecommercialproductionbegins istheestimatedunitrecovery.Thisunitrecoveryisthedifferencebetweentheinitialgasinplace andthegasremaininginthereservoiratthetimeofabandonmentandrepresentsthetotalgasthat canbeproducedfromthereservoir.Thissameinformationisoftenexpressedasarecoveryfactor, showingthepercentoftheinitialgasinplacethatcanbeproduced.Thesepiecesofinformation arecrucialformakingtheeconomicdecisionbehindthedevelopmentofahydrocarbonreservoir. 87 88 Chapter 4 • Single-Phase Gas Reservoirs Therecoveryfactoritselfisdependentontheproductionmechanismforthereservoir.Two mainmechanismsingasreservoirswillbediscussedinthischapter.Theyaregas drive,whichis theexpansionofthegasinthereservoirduetoadropinreservoirpressureasgasisbeingproduced, andwaterdrive,whichistheencroachmentofwaterinthereservoirduetocontactwithanaquifer.Inthecaseofagasdrive,thereisneitherwaterencroachmentintonorwaterproductionfrom thereservoirofinterest,andthereservoirissaidtobevolumetric.Thischapterwillalsoprovide adescriptionoftwomethodsthatareusedtodeterminetheinitialgasinplace.Thefirstofthese methods uses geological, geophysical, and fluid property data to estimate volumes of gas. The secondmethodusesthematerialbalanceequationderivedinChapter3. 4.2 Calculating Hydrocarbon in Place Using Geological, Geophysical, and Fluid Property Data Inorderforthereservoirengineertocalculatetheamountofhydrocarboninplacefromgeological information,thereservoirbulkvolumemustfirstbecalculated.Manymethodsexisttoestimatethe reservoirbulkvolumebutonlytwowillbediscussedhere. Thefirstmethodinvolvesthereservoirengineerusingwelllogs,coredata,welltestdata,and two-dimensionalseismicdatatoestimatethebulkvolume.1,2Fromthisinformation,theengineergeneratesdigitalsubsurfaceandisopachmapsofthereservoirinquestion.Thesemapsarethenusedin computerprogramstoestimateavolumeforagivenhydrocarbon,eithergasoroil,inplace.3 A subsurface contour map shows lines connecting points of equal elevations on the topofamarkerbedandthereforeshowsgeologicstructure.Anetisopachmapshowslines connectingpointsofequalnetformationthickness,andtheindividuallinesconnectingpoints ofequalthicknessarecalledisopach lines.Thecontourmapisusedinpreparingtheisopach maps when there is an oil-water, gas-water, or gas-oil contact. The contact line is the zero isopachline.Thevolumeisobtainedbyplanimeteringtheareasbetweentheisopachlinesof theentirereservoiroroftheindividualunitsunderconsideration.Theprincipalproblemsin preparingamapofthistypearetheproperinterpretationofnetsandthicknessfromthewell logsandtheoutliningoftheproductiveareaofthefieldasdefinedbythefluidcontacts,faults, orpermeabilitybarriersonthesubsurfacecontourmap.Whentheformationisratheruniformlydevelopedandthereisgoodwellcontrol,theerrorinthenetbulkreservoirvolumeshould notexceedafewpercentagepoints. Asecondmethodofcalculatinghydrocarboninplaceinvolvescomputermodelingandis becoming increasingly common with the advancement of three-dimensional seismic data. This approachbeginswiththecollectionofthree-dimensionalseismicdataviaanarrayoftransmitters ofreceivers.Thesedataarecollected,processed,anddisplayedinadigitalthree-dimensionalgeologicmodel. Thisprocessstillrequireswelllogstocalibratetheseismicdata,buttheincreaseinseismic dataobtained(fromatwo-dimensionalsurveytoathree-dimensionalsurvey)resultsintheability todelineatethereservoirwithfewerwellsdrilled.Modernworkstationprogramsareusedtoenabletransferoftheresultinggeologicmodeltoanumericalreservoirsimulatorinwhichthebulk volumeiscalculated. 4.2 Calculating Hydrocarbon in Place 89 Oncetheengineerhasdeterminedthebulkvolumeofthereservoir,calculationsforhydrocarboninplacecanthenbemade.Themethodsdiscussedinthepreviousparagraphsapplytoboth gasandoilreservoirsandwillbementionedbrieflyagaininChapter6.Thefollowingdiscussion illustratesthecalculationofhydrocarboninplaceforagasreservoir. ThestandardcubicfeetofgasinareservoirwithagasporevolumeofVgft3issimplyVg/Bg, whereBgisexpressedinunitsofcubicfeetperstandardcubicfoot.AsthegasvolumefactorBg changeswithpressure(seeEq.[2.16]),thegasinplacealsochangesasthepressuredeclines.The gasporevolumeVgmayalsobechanging,owingtowaterinfluxintothereservoir.Thegaspore volumeisrelatedtothebulk,ortotal,reservoirvolumebytheaverageporosityφandtheaverage connatewaterSw.ThebulkreservoirvolumeVbiscommonlyexpressedinacre-feet,andthestandardcubicfeetofgasinplace,G,isgivenby G= 43, 560Vbφ (1 − Sw ) Bg (4.1) ThearealextentoftheBellFieldgasreservoirwas1500acres.Theaveragethicknesswas40ft, sotheinitialbulkvolumewas60,000ac-ft.Averageporositywas22%,andaverageconnatewater was23%.Bgattheinitialreservoirpressureof3250psiawascalculatedtobe0.00533ft3/SCF. Therefore,theinitialgasinplacewas G=43,560×60,000×0.22×(1–0.23)÷0.00533 =83.1MMMSCF Becausethegasvolumefactoriscalculatedusing14.7psiaand60°Fasstandardconditions,the initialgasinplaceisalsoexpressedattheseconditions. Becausetheformationvolumefactorisafunctionoftheaveragereservoirpressure,another probleminanycalculationofbulkhydrocarbonvolumeisthatofobtainingtheaveragereservoir pressureatanytimeafterinitialproduction.Figure4.1isastaticreservoirpressuresurveyofthe JonessandintheSchulerField.4Becauseofthelargereservoirpressuregradientfromeasttowest, someaveragingtechniquemustbeusedtoobtainanaveragereservoirpressure.Thiscanbecalculatedaseitheranaveragewellpressure,averagearealpressure,oraveragevolumetricpressure, asfollows: n Wellaveragepressure= ∑ pi 0 n (4.2) n Arealaveragepressure= ∑ pi Ai 0 n ∑ Ai 0 (4.3) Chapter 4 • Single-Phase Gas Reservoirs 1700 90 1650 1685 1660 1595 1405 1620 1510 Figure 4.1 1200 1150 1590 1655 1300 1685 1675 1250 1700 1550 1695 1695 1350 1685 1500 1450 1400 1600 1685 1275 1155 Reservoir pressure survey showing isobaric lines drawn from the measured bottom-hole pressures (in units of psia; after Kaveler, trans. AlME).4 n Volumetricaveragepressure= ∑ pi Ai hi 0 n ∑ Ai hi (4.4) 0 wherenisthenumberofwellsinEq.(4.2)andthenumberofreservoirunitsinEqs.(4.3)and(4.4). Sinceobtainingtheaveragepressureofthehydrocarboncontentsistheimportantpiece ofdata,thevolumetricaverage,Eq.(4.4),shouldbeusedinthecalculationsforbulkhydrocarbonvolume.Wherethepressuregradientsinthereservoiraresmall,theaveragepressures obtainedwithEqs.(4.2)and(4.3)willbeveryclosetothevolumetricaverage.Wherethegradientsarelarge,theremaybeconsiderabledifferences.Forexample,theaveragevolumetric pressureoftheJonessandsurveyinFig.4.1is1658psia,comparedwith1598psiaforthe wellaveragepressure. ThecalculationsinTable4.1showhowtheaveragepressuresareobtained.Thefiguresinthe thirdcolumnaretheestimateddrainageareasofthewells,whichinsomecasesvaryfromthewell spacingbecauseofthereservoirlimits.Owingtothemuchsmallergradients,thethreeaveragesare muchclosertogetherthaninthecaseoftheJonessand. Mostengineersprefertoprepareanisobaricmapandplanimetertheareasbetweentheisobariclinesandthenusecomputersoftwaretocalculatetheaveragevolumetricpressure. 4.2 Calculating Hydrocarbon in Place 91 Table 4.1 Calculation of Average Reservoir Pressure Well number Pressure (psia) Drainage area (acres) p×A Estimated standard thickness (ft) p×A×h A×h 1 2750 160 440,000 20 8,800,000 3200 2 2680 125 335,000 25 8,375,000 3125 3 2840 190 539,600 26 14,029,600 4940 4 2700 145 391,500 31 12,136,500 4495 Total 10,970 620 1,706,100 43,341,100 15,760 Wellaveragepressure= 10, 970 = 2743 psia 4 1, 706, 100 = 2752 psia 620 Arealaveragepressure= Volumetricaveragepressure= 4.2.1 43, 341, 100 = 2750 psia 15, 760 Calculating Unit Recovery from Volumetric Gas Reservoirs Inmanygasreservoirs,particularlyduringthedevelopmentperiod,thebulkvolumeisnotknown. Inthiscase,itisbettertoplacethereservoircalculationsonaunitbasis,usually1ac-ftofbulk reservoirrock.Thisoneunit,or1ac-ft,ofbulkreservoirrockcontains Connatewater:43,560× φ × Swft3 Reservoirgasvolume:43,560× φ ×(1–Sw)ft3 Reservoirporevolume:43,560× φft3 Theinitialstandardcubicfeetofgasinplaceintheunitis G= 43, 560(φ )(1 − Swi ) SCF/ac-ft Bgi (4.5) Gisinstandardcubicfeet(SCF)whenthegasvolumefactorBgiisincubicfeetperstandardcubic foot(seeEq.[2.16]).Thestandardconditionsarethoseusedinthecalculationofthegasvolume factor,andtheymaybechangedtoanyotherstandardbymeansoftheidealgaslaw.Theporosity, φ,isexpressedasafractionofthebulkvolumeandtheinitialconnatewater,Swi,asafractionofthe Chapter 4 92 • Single-Phase Gas Reservoirs porevolume.Forareservoirundervolumetriccontrol,thereisnochangeintheinterstitialwater, sothereservoirgasvolumeremainsthesame.IfBgaisthegasvolumefactorattheabandonment pressure,thenthestandardcubicfeetofgasremainingatabandonmentis Ga = 43, 560(φ )(1 − Swi ) SCF/ac-ft Bga (4.6) Unitrecoveryisthedifferencebetweentheinitialgasinplaceandthatremainingatabandonment pressure(i.e.,thatproducedatabandonmentpressure),or 1 1 Unitrecovery=43,560(φ)(1–Swi) − SCF/ac-ft Bgi Bga (4.7) Theunitrecoveryisalsocalledtheinitial unit reserve,whichisgenerallylowerthantheinitialunit in-placegas.Theremainingreserveatanystageofdepletionisthedifferencebetweenthisinitial reserveandtheunitproductionatthatstageofdepletion.Thefractionalrecoveryorrecoveryfactor expressedinapercentageoftheinitialin-placegasis 1 1 100 − 100(G − Ga ) Bgi Bga % Recoveryfactor= = 1 G Bgi (4.8) or Bgi Recoveryfactor=100 1 − Bga Experiencewithvolumetricgasreservoirsindicatesthattherecoveryfactorwillrangefrom80%to 90%.Somegaspipelinecompaniesuseanabandonmentpressureof100psiper1000ftofdepth. ThegasvolumefactorintheBellGasFieldatinitialreservoirpressureis0.00533ft3/SCF, andat500psia,itis0.03623ft3/SCF.Theinitialunitreserveorunitrecoverybasedonvolumetric performanceatanabandonmentpressureof500psiais 1 1 − Unitrecovery=43,560×0.22×(1–0.23)× 0 . 00533 0 . 03623 =1180MSCF/ac-ft 0.00533 Recoveryfactor= 1 − 0.03623 =85% 4.2 Calculating Hydrocarbon in Place 93 Theserecoverycalculationsarevalidprovidedtheunitneitherdrainsnorisdrainedbyadjacentunits. 4.2.2 Calculating Unit Recovery from Gas Reservoirs under Water Drive Underinitialconditions,oneunit(1ac-ft)ofbulkreservoirrockcontains Connatewater:43,560× φ × Swift3 Reservoirgasvolume:43,560× φ ×(1–Swi)ft3 Surfaceunitsofgas:43,560× φ ×(1–Swi)÷ BgiSCF Inmanyreservoirsunderwaterdrive,thepressuresuffersaninitialdecline,afterwhichwaterentersthereservoiratarateequaltotheproductionrateandthepressurestabilizes.Inthiscase,the stabilizedpressureistheabandonmentpressure.IfBgaisthegasvolumefactorattheabandonment pressureandSgristheresidualgassaturation,expressedasafractionoftheporevolume,afterwater invadestheunit,thenunderabandonmentconditions,aunit(1ac-ft)ofthereservoirrockcontains Watervolume:43,560× φ ×(1–Sgr)ft3 Reservoirgasvolume:43,560× φ × Sgrft3 Surfaceunitsofgas:43,560× φ × Sgr ÷ BgaSCF Unitrecoveryisthedifferencebetweentheinitialandtheresidualsurfaceunitsofgas,or 1 − Swi Sgr UnitrecoveryinSCF/ac-ft=43,560(φ) − Bga Bgi (4.9) Therecoveryfactorexpressedinapercentageoftheinitialgasinplaceis 1 − Swi Sgr − 100 Bga Bgi Recoveryfactor = 1 − Swi Bgi (4.10) SupposetheBellGasFieldisproducedunderawaterdrivesothatthepressurestabilizesat1500 psia.Iftheresidualgassaturationis24%andthegasvolumefactorat1500psiais0.01122ft3/SCF, thentheinitialunitreserveorunitrecoveryis 0.24 (1 − 0.23) − Unitrecovery=43,560×0.22× 0.00533 0.0112 =1180MSCF/ac-ft Chapter 4 94 • Single-Phase Gas Reservoirs Therecoveryfactorundertheseconditionsis 0.24 1 − 0.23 100 − 0.00533 0.0112 = 85% Recoveryfactor = 1 − 0.23 0.00533 Undertheseparticularconditions,therecoverybywaterdriveisthesameastherecoverybyvolumetricdepletion,illustratedinsection4.3.Ifthewaterdriveisveryactiveand,asaresult,thereis essentiallynodeclineinreservoirpressure,unitrecoveryandtherecoveryfactorbecome Unitrecovery=43,560× φ ×(1–Swi – Sgr)÷ BgiSCF/ac-ft Recoveryfactor= 100(1 − Swi − Sgr ) (1 − Swi ) % (4.11) (4.12) FortheBellGasField,assumingaresidualgassaturationof24%, Unitrecovery=43,560×0.22×(1–0.23–0.24)÷0.00533 =953MSCF/ac-ft Recoveryfactor= 100(1 − 0.23 − 0.24 ) (1 − 0.23) =69% Becausetheresidualgassaturationisindependentofthepressure,therecoverywillbegreaterfor thelowerstabilizationpressure. Theresidualgassaturationcanbemeasuredinthelaboratoryonrepresentativecoresamples. Table4.2givestheresidualgassaturationsthatweremeasuredoncoresamplesfromanumber ofproducinghorizonsandonsomesyntheticlaboratorysamples.Thevalues,whichrangefrom 16%to50%andaveragenear30%,helptoexplainthedisappointingrecoveriesobtainedinsome water-drivereservoirs.Forexample,agasreservoirwithaninitialwatersaturationof30%anda residualgassaturationof35%hasarecoveryfactorofonly50%ifproducedunderanactivewater drive(i.e.,wherethereservoirpressurestabilizesneartheinitialpressure).Whenthereservoirpermeabilityisuniform,thisrecoveryfactorshouldberepresentative,exceptforacorrectiontoallow fortheefficiencyofthedrainagepatternandwaterconingorcusping.Whentherearewell-defined continuousbedsofhigherandlowerpermeability,thewaterwilladvancemorerapidlythroughthe morepermeablebedssothatwhenagaswellisabandonedowingtoexcessivewaterproduction, considerableunrecoveredgasremainsinthelesspermeablebeds.Becauseofthesefactors,itmay beconcludedthatgenerallygasrecoveriesbywaterdrivearelowerthanbyvolumetricdepletion; 4.2 Calculating Hydrocarbon in Place 95 however, the same conclusion does not apply to oil recovery, which is discussed separately. Water-drivegasreservoirsdohavetheadvantageofmaintaininghigherflowingwellheadpressures andhigherwellratescomparedwithdepletiongasreservoirs.Thisisdue,ofcourse,tothemaintenanceofhigherreservoirpressureasaresultofthewaterinflux. Incalculatingthegasreserveofaparticularleaseorunit,thegasthatcanberecoveredby thewell(s)ontheleaseisimportantratherthanthetotalrecoverablegasinitiallyunderlyingthe lease,someofwhichmayberecoveredbyadjacentwells.Involumetricreservoirswheretherecoverablegasbeneatheachlease(well)isthesame,therecoverieswillbethesameonlyifallwells areproducedatthesamerate.Ontheotherhand,ifwellsareproducedatequalrateswhenthegas beneaththeleases(wells)varies,asfromvariableformationthickness,thecalculatedinitialgas reserveofthelease,wheretheformationisthicker,willbelessthantheinitialactualrecoverable gasunderlyingthelease. Inwater-drivengasreservoirs,whenthepressurestabilizesneartheinitialreservoirpressure, thelowestwellonstructurewilldivideitsinitialrecoverablegaswithallupdipwellsinlinewith it.Forexample,ifthreewellsinlinealongthediparedrilledattheupdipedgeoftheirunits,which arepresumedequal,andiftheyallproduceatthesameratewiththesameproducinglife,thenthe lowestwellonstructurewillrecoverapproximatelyone-thirdofthegasinitiallyunderlyingit.If thewellisdrilledfurtherdownstructurenearthecenteroftheunit,itwillrecoverstillless.Ifthe Table 4.2 Residual Gas Saturation after Waterflood as Measured on Core Plugs (after Geffen, Parish, Haynes, and Morse)5 Residual gas saturation, percentage of pore space Remarks Unconsolidatedsand 16 (13-ftcolumn) Slightlyconsolidated sand(synthetic) 21 (1core) 17 (1core) Porous material Syntheticconsolidated materials Consolidatedsandstones Formation Selasporcelain Nortonalundum 24 (1core) Wilcox 25 (3cores) Frio 30 (1core) Nellie Bly 30–36 (12cores) Frontier 31–34 (3cores) Springer 33 (3cores) Frio 30–38 (14cores) (Average34.6) Limestone Torpedo 34–37 (6cores) Tensleep 40–50 (4cores) Canyonreef 50 (2cores) Chapter 4 96 • Single-Phase Gas Reservoirs pressurestabilizesatsomepressurebelowtheinitialreservoirpressure,therecoveryfactorwill beimprovedforthewellslowonstructure.Example4.1showsthecalculationoftheinitialgas reserveofa160-acreunitbyvolumetricdepletion,partialwaterdrive,andcompletewaterdrive. Example 4.1 Calculating the Initial Gas Reserve of a 160-acre Unit of the Bell Gas Field by Volumetric Depletion and under Partial and Complete Water Drive Given Averageporosity=22% Connatewater=23% Residualgassaturationafterwaterdisplacement=34% Bgi=0.00533ft3/SCFatpi=3250psia Bg=0.00667ft3/SCFat2500psia Bga=0.03623ft3/SCFat500psia Area=160acres Netproductivethickness=40ft Solution Porevolume=43,560×0.22×160×40=61.33×106ft3 Initialgasinplaceis G1=61.33×106 ×(1–0.23)÷0.00533=8860MMSCF Gasinplaceaftervolumetricdepletionto2500psiais G2=61.33×106 ×(1–0.23)÷0.00667=7080MMSCF Gasinplaceaftervolumetricdepletionto500psiais G3=61.33×106 ×(1–0.23)÷0.03623=1303MMSCF Gasinplaceafterwaterinvasionat3250psiais G4=61.33×106 ×0.34÷0.00533=3912MMSCF Gasinplaceafterwaterinvasionat2500psiais G5=61.33×106 ×0.34÷0.00667=3126MMSCF 4.2 Calculating Hydrocarbon in Place 97 Initialreservebydepletionto500psiais G1 – G3=(8860–1303)×106=7557MMSCF Initialreservebywaterdriveat3250psiais G1 – G4=(8860–3912)×106=4948MMSCF Initialreservebywaterdriveat2500psiais (G1 – G5)=(8860–3126)×106=5734MMSCF Ifthereisoneupdipwell,theinitialreservebywaterdriveat3250psiais 1 2 (G1 – G4)= 12 (8860–3912)×106=2474MMSCF Therecoveryfactorscalculatetobe85%,65%,and56%forthecasesofnowaterdrive, partialwaterdrive,andfullwaterdrive,respectively.Theserecoveriesarefairlytypicalandcan beexplainedinthefollowingway.Aswaterinvadesthereservoir,thereservoirpressureismaintainedatahigherlevelthanifwaterencroachmentdidnotoccur.Thisleadstohigherabandonmentpressuresforwater-drivereservoirs.Becausethemainmechanismofproductioninagas reservoiristhatofdepletionorgasexpansion,recoveriesarelower,asshowninExample4.1. Agarwal,Al-Hussainy, and Ramey conducted a theoretical study and showed that gas recoveriesincreasedwithincreasingproductionratesfromwater-drivereservoirs.6Thistechnique of“outrunning”thewaterhasbeenattemptedinthefieldandhasbeenfoundsuccessful.Matthes, Jackson, Schuler, and Marudiak showed that ultimate recovery increased from 69% to 74% by increasingthefieldproductionratefrom50to75MMSCF/DintheBierwangFieldinWestGermany.7Lutes,Chiang,Brady,andRossenreportedan8.5%increaseinultimaterecovery,withan increasedproductionrateinastrongwater-driveGulfCoastgasreservoir.8 A second technique used in the field is the coproduction technique discussed byArcaro andBassiouni.9Thecoproductiontechniqueisdefinedasthesimultaneousproductionofgasand water.Inthecoproductionprocess,asdowndipwellsbegintobewateredout,theyareconverted tohigh-ratewaterproductionwells,whiletheupdipwellsaremaintainedongasproduction.This techniqueenhancestheproductionofgasbyseveralmethods.First,thehigh-ratedowndipwater wellsactasapressuresinkforthewaterbecausethewaterisdrawntothesewells.Thisretards theinvasionofwaterintoproductivegaszonesinthereservoir,thereforeprolongingusefulproductivelifetothesezones.Second,thehigh-rateproductionofwaterlowerstheaveragepressure inthereservoir,allowingformoregasexpansionandthereforemoregasproduction.Third,when theaveragereservoirpressureislowered,immobilegasinthewater-sweptportionofthereservoir could become mobile.The coproduction technique performs best before the reservoir is totally Chapter 4 98 • Single-Phase Gas Reservoirs invadedbywater.ArcaroandBassiounireportedtheimprovementofgasproductionfrom62%to 83%intheLouisianaGulfCoastEugeneIslandBlock305Reservoirbyusingthecoproduction techniqueinsteadoftheconventionalproductionapproach.Water-drivereservoirsarediscussedin muchmoredetailinChapter9. 4.3 Calculating Gas in Place Using Material Balance Intheprevioussections,theinitialgasinplacewascalculatedonaunitbasisof1ac-ftofbulk productiverock,giveninformationontheporosityandconnatewater.Tocalculatetheinitialgasin placeonanyparticularportionofareservoir,itisnecessarytoknow,inaddition,thebulkvolume ofthatportionofthereservoir.Iftheporosity,connatewater,and/orbulkvolumesarenotknown withanyreasonableprecision,themethodsdescribedcannotbeused.Inthiscase,thematerial balancemethodmaybeusedtocalculatetheinitialgasinplace;however,thismethodisapplicable onlytothereservoirasawholebecauseofthemigrationofgasfromoneportionofthereservoir toanotherinbothvolumetricandwater-drivereservoirs. ThegeneralmaterialbalanceequationforagasreservoirisderivedinChapter3: cw Swi + c f G(Bg – Bgi) + GBgi 1 − Swi Δp + We = G p Bg + BwW p (3.10) Equation(3.10)couldhavebeenderivedbyapplyingthelawofconservationofmasstothereservoirandassociatedproduction. Formostgasreservoirs,thegascompressibilitytermismuchgreaterthantheformationand watercompressibilities,andthesecondtermontheleft-handsideofEq.(3.10)becomesnegligible: G(Bg – Bgi)+We = GpBg + BwWp (4.13) Whenreservoirpressuresareabnormallyhigh,thistermisnotnegligibleandshouldnotbeignored.Thissituationisdiscussedinalatersectionofthischapter. 4.3.1 Material Balance in Volumetric Gas Reservoirs Foravolumetricgasreservoir,Eq.(4.13)canbereducedtoasimpleapplicationofastraight lineinvolvingthegasproduced,itscomposition,andthereservoirpressure.Thisrelationship isroutinelyusedbyreservoirengineerstopredictrecoveriesfromvolumetricreservoirs.Since thereisneitherwaterencroachmentnorwaterproductioninthistypeofareservoir,Eq.(4.13) reducesto G(Bg – Bgi)=GpBg (4.14) UsingEq.(2.15)andsubstitutingexpressionsforBg and BgiintoEq.(4.14),thefollowingisobtained: 4.3 Calculating Gas in Place Using Material Balance 99 p zT p zT p zT G sc − G sc i i = G p sc Tsc p Tsc p Tsc pi (4.15) Notingthatproductionisessentiallyanisothermalprocess(i.e.,thereservoirtemperatureremains constant),thenEq.(4.15)isreducedto z z z G − G i = Gp p p pi Thiscanberearrangedas p p p = − i Gp + i z zi G zi (4.16) Becausepi, zi, and Gareconstantsforagivenreservoir,Eq.(4.16)suggeststhataplotofp/zasthe ordinateversusGpastheabscissawouldyieldastraightline,with 5000 4000 3000 Volumetric Gp vs p/z Initial gas in place Pressure or p/z Water drive 2000 Volumetric Gp vs p 1000 Wrong extrapolation 0 0 Figure 4.2 1 2 3 4 5 Cumulative production, MMM SCF 6 7 Comparison of theoretical values of p and p/z plotted versus cumulative production from a volumetric gas reservoir. Chapter 4 100 slope = − • Single-Phase Gas Reservoirs pi zi G yintercept = pi zi ThisplotisshowninFig.4.2. Ifp/zissetequaltozero,whichwouldrepresenttheproductionofallthegasfromareservoir,thenthecorrespondingGpequalsG,theinitialgasinplace.Theplotcouldalsobeextrapolatedtoanyabandonmentp/ztofindtheinitialreserve.Usuallythisextrapolationrequiresatleast 3yearsofaccuratepressuredepletionandgasproductiondata. Figure4.2alsocontainsaplotofcumulativegasproductionGpversuspressure.AsindicatedbyEq.(4.16),thisisnotlinear,andextrapolationsfromthepressure-productiondatamay beinconsiderableerror.Becausetheminimumvalueofthegasdeviationfactorgenerallyoccurs near2500psia,theextrapolationswillbelowforpressuresabove2500psiaandhighforpressuresbelow2500psia.Equation(4.16)maybeusedgraphically,asshowninFig.4.2,tofindthe initialgasinplaceorthereservesatanypressureforanyselectedabandonmentpressure.Forexample,at1000psia(orp/z=1220)abandonmentpressure,theinitialreserveis4.85MMMSCF. At2500psia(orp/z=3130),the(remaining)reserveis4.85less2.20—thatis,2.65MMMSCF. 4.3.2 Material Balance in Water-Drive Gas Reservoirs Inwater-drivereservoirs,therelationbetweenGp and p/zisnotlinear,ascanbeseenbyaninspectionofEqs.(4.13)and(4.16).Becauseofthewaterinflux,thepressuredropslessrapidlywith productionthanundervolumetriccontrol,asshownintheuppercurveofFig.4.2.Consequently, theextrapolationtechniquedescribedforvolumetricreservoirsisnotapplicable.Also,wherethere iswaterinflux,theinitialgasinplacecalculatedatsuccessivestagesofdepletion,assumingno waterinflux,takesonsuccessivelyhighervalues,whereaswithvolumetricreservoirsthecalculated valuesoftheinitialgasshouldremainsubstantiallyconstant. Equation(4.13)maybeexpressedintermsoftheinitialporevolume,Vi,byrecognizingthat Vi= GBgiandusingEq.(2.15)forBg and Bgi: z f T pi z f T p sc G p − 1 = Vi + BwW p − We p f Tsc p f Zi T (4.17) Forvolumetricreservoirs,discussedintheprevioussection,thisequationcanbereducedandrearrangedtogive psc G p Tsc = piVi p f Vi − zi T zfT (4.18) Examples4.2,4.3,and4.4illustratetheuseofthevariousequationsthatwehavedescribed ingasreservoircalculations. 4.3 Calculating Gas in Place Using Material Balance 101 Example 4.2 Calculating the Initial Gas in Place and the Initial Reserve of a Gas Reservoir from Pressure-Production Data for a Volumetric Reservoir Given Basepressure=15.025psia Initialpressure=3250psia Reservoirtemperature=213°F Standardpressure=15.025psia Standardtemperature=60°F Cumulativeproduction=1.00×109SCF Averagereservoirpressure=2864psia Gasdeviationfactorat3250psia=0.910 Gasdeviationfactorat2864psia=0.888 Gasdeviationfactorat500psia=0.951 Solution SolveEq.(4.18)forthereservoirgasporevolumeVi: 15.023 × 1.00 × 10 9 3250 × Vi 2864 Vi − = 520 0.910 × 673 0.888 × 673 Vi=56.17MMft3 Theinitialgasinplacebytherealgaslawis piVi Tsc 3250 × 56.17 × 10 6 × 520 × = 0.910 × 673 × 15..025 zi T psc G= =10.32MMMSCF Thegasremainingat500-psiaabandonmentpressureis Ga = paVi Tsc 500 × 56.17 × 10 6 × 520 × = 0.951 × 673 × 15..025 za T psc =1.52MMMSCF Theinitialgasreservebasedona500-psiaabandonmentpressureisthedifferencebetweenthe initialgasinplaceandthegasremainingat500psia,or Gr = G – Ga =(10.32–1.52)×109 =8.80MMMSCF Chapter 4 102 • Single-Phase Gas Reservoirs Example4.3illustratestheuseofequationstocalculatethewaterinfluxwhentheinitialgas inplaceisknown.Italsoshowsthemethodofestimatingtheresidualgassaturationoftheportion ofthereservoirinvadedbywater,atwhichtimeareliableestimateoftheinvadedvolumecanbe made.Thisiscalculatedfromtheisopachmap,theinvadedvolumebeingdelineatedbythosewells thathavegonetowaterproduction.TheresidualgassaturationcalculatedinExample4.3includes thatportionofthelowerpermeabilityrockwithintheinvadedareathatactuallymaynothavebeen invadedatall,thewellshavingbeen“drowned”bywaterproductionfromthemorepermeablebeds oftheformation.Nevertheless,itisstillinterpretedastheaverageresidualgassaturation,which maybeappliedtotheuninvadedportionofthereservoir. Example 4.3 Calculating Water Influx and Residual Gas Saturation in Water-Drive Gas Reservoirs Given Bulkreservoirvolume,initial=415.3MMft3 Averageporosity=0.172 Averageconnatewater=0.25 Initialpressure=3200psia Bgi=0.005262ft3/SCF,14.7psiaand60°F Finalpressure=2925psia Bgf=0.005700ft3/SCF,14.7psiaand60°F Cumulativewaterproduction=15,200bbl(surface) Bw=1.03bbl/surfacebbl Gp=935.4MMSCFat14.7psiaand60°F Bulkvolumeinvadedbywaterat2925psia=13.04MMft3 Solution Initialgasinplace = G = 415.3 × 10 6 × 0.172 × (1 − 0.25 ) 0.005262 =10,180MMSCFat14.7psiaand60°F SubstituteinEq.(4.13)tofindWe: We=935.4×106 ×0.005700–10,180×106 (0.005700–0.005262)+15,200×1.03×5.615 =960,400ft3 Thismuchwaterhasinvaded13.04MMft3ofbulkrockthatinitiallycontained25%connate water.Thenthefinalwatersaturationofthefloodedportionofthereservoiris 4.3 Calculating Gas in Place Using Material Balance Sw = = 103 Connatewater+Water influx–Producedwaterr Pore space (13.04 × 10 6 × 0.172 × 0.25)+960,400–15,200 × 1.03 = 0.67 or67% 13.04 × 10 6 × 0.172 ThentheresidualgassaturationSgris33%. Example 4.4. Using the p/z Plot to Estimate Cumulative Gas Production Adrygasreservoircontainsgasofthefollowingcomposition Mole fraction Methane 0.75 Ethane 0.20 n-Hexane 0.05 Theinitialreservoirpressurewas4200psia,withatemperatureof180°F.Thereservoirhasbeen producingforsometime.Twopressuresurveyshavebeenmadeatdifferenttimes: p/z (psia) Gp (MMM SCF) 4600 0 3700 1 2800 2 (a) Whatwillbethecumulativegasproducedwhentheaveragereservoirpressurehasdropped to2000psia? (b) Assumingthereservoirrockhasaporosityof12%,thewatersaturationis30%,andthe reservoirthicknessis15ft,howmanyacresdoesthereservoircover? Solution Pc Tc YPc YTc Methane 0.75 673.1 343.2 504.8 257.4 Ethane 0.20 708.3 504.8 141.7 110.0 n-Hexane 0.05 440.1 914.2 22.0 45.7 668.5 413.1 Total Chapter 4 104 • Single-Phase Gas Reservoirs (a) TogetGpat2000psia,calculatezandthep/z.Usepseudocriticalproperties. pr = 2000 = 2.99 668.5 Tr = 640 = 1.55 413.1 z=0.8 p /z = 2000 = 2500 0.8 AlinearregressionofthedataplottedinFig.4.3yieldsthefollowingequationforthebest straightlinethroughthedata: p/z=–9(10)–7Gp+4600 5000 4000 p/z 3000 2000 1000 0 0 0.5 1.0 1.5 Gp MMM SCF Figure 4.3 p/z versus Gp for Example 4.4. 2.0 2.5 4.4 The Gas Equivalent of Produced Condensate and Water 105 Substitutingavalueofp/z=2500inthisequationyields 2500=–9(10)–7Gp+4600 Gp=2.33(10)9SCFor2.33MMMSCF (b) Substitutingavalueofp/z=0intothestraight-lineequationwouldyieldtheamountofproducedgasifalloftheinitialgaswereproduced;therefore,theGpatthisp/zisequaltothe initialgasinplace. 0=–9(10)–7Gp+4600 Gp(p/z=0)=G=5.11(10)9SCFor5.11MMMSCF RecognizingthatVi = GBgiandthatBgi=0.02829(zi/pi)T, 0.02829(180 + 460 ) 6 3 Vi = GBgi = 5.11(10 )9 = 20.11(10 ) ft 4600 Also, Vi = Ah φ(1–Swi) A= 4.4 20.1(10 )6 = 15.95(10 )6 ft 2 15(0.12 )(1 − 0.30 ) or 366 acres The Gas Equivalent of Produced Condensate and Water Inthestudyofgasreservoirsintheprecedingsection,itwasimplicitlyassumedthatthefluidinthe reservoiratallpressuresaswellasonthesurfacewasinasingle(gas)phase.Mostgasreservoirs, however,producesomehydrocarbonliquid,commonlycalledcondensate,intherangeofafewtoa hundredormorebarrelspermillionstandardcubicfeet.Solongasthereservoirfluidremainsina single(gas)phase,thecalculationsoftheprevioussectionsmaybeused,providedthecumulativegas productionGpismodifiedtoincludethecondensateliquidproduction.Ontheotherhand,ifahydrocarbonliquidphasedevelopsinthereservoir,themethodsoftheprevioussectionsarenotapplicable, andtheseretrograde,gas-condensatereservoirsmustbetreatedspecially,asdescribedinChapter5. The reservoir gas production Gp used in the previous sections must include the separator gasproduction,thestock-tankgasproduction,andthestock-tankliquidproductionconvertedto itsgasequivalent(GE).Figure4.4illustratestwocommonseparationschemes,oneofwhich,the two-stagesystem,showninFig.4.4(b),isdiscussedinChapter1.Figure4.4(a)showsathree-stage separationsystemwithaprimaryseparator,asecondaryseparator,andastocktank.Thewellfluid isintroducedintotheprimaryseparatorwhere,likethetwo-stagesystem,mostoftheproducedgas Chapter 4 106 Single-Phase Gas Reservoirs Gss Gps Well fluid • Primary separator Gp(surf) Gst Secondary separator Stock tank Np (a) Three-stage separation system Gps Well fluid Primary separator Gst Gp(surf) Stock tank Np (b) Two-stage separation system Figure 4.4 Schematic representation of surface separation systems. isobtained.Theliquidfromtheprimaryseparatoristhensenttothesecondaryseparatorwherean additionalamountofgasisobtained.Theliquidfromthesecondaryseparatoristhenflashedinto thestocktank.Theliquidfromthestocktank,Np,andanygasfromthestocktankareaddedtothe primaryandsecondarygastoobtainthetotalproducedsurfacegas,Gp(surf). Theproducedhydrocarbonliquidisconvertedtoitsgasequivalent,assumingitbehavesas anidealgaswhenvaporizedintheproducedgas.Taking14.7psiaand60°Fasstandardconditions, thegasequivalentofonestock-tankbarrelofcondensateliquidis GE = V = nR ' Tsc 350.5γ o (10.73)(520 ) γ = = 133, 000 o psc M wo (14.7 ) M wo (4.19) Thegasequivalentofonebarrelofcondensateofspecificgravityof0.780(water=1.00)and molecularweight138is752SCF.ThespecificgravitymaybecalculatedfromtheAPIgravity.If themolecularweightofthecondensateisnotmeasured,asbythefreezingpointdepressionmethod,itcanbeestimatedusingEq.(4.20): M wo = 5954 42.43γ o = ρo, API − 8.811 1.008 − γ o (4.20) ThetotalgasequivalentforNpSTBofcondensateproductionisGE(NP).Thetotalreservoir gasproduction,Gp,isgivenbyEq.(4.21)forathree-stageseparationsystemandbyEq.(4.22)for atwo-stageseparationsystem: 4.5 Gas Reservoirs as Storage Reservoirs 107 Gp = Gp(surf) + GE(Np)=Gps + Gss + Gst + GE(Np) (4.21) Gp = Gp(surf) + GE(Np) = Gps + Gst + GE(Np) (4.22) Whenwaterisproducedonthesurfaceasacondensatefromthegasphaseinthereservoir, itisfreshwaterandshouldbeconvertedtoagasequivalentandaddedtothegasproduction.Since thespecificgravityofwateris1.00anditsmolecularweightis18,itsgasequivalentis GEw = nR ' Tsc 350 × 1.00 10.73 × 520 = × psc 18 14.7 =7390SCF/surfacebarrel StudiesbyMcCarthy,Boyd,andReidindicatethatthewatervaporcontentofreservoir gases at usual reservoir temperatures and usual initial reservoir pressures is in the range of a fractionofonebarrelpermillionstandardcubicfeetofgas.10ProductiondatafromaGulfCoast gasreservoirshowaproductionof0.64barrelofwaterpermillionstandardcubicfeetcompared withareservoircontentofabout1.00bbl/MMSCFusingthedataofMcCarthy,Boyd,andReid. Thedifferenceispresumablythatwaterremaininginthevaporstateatseparatortemperatureand pressure,mostofwhichmustberemovedbydehydrationtoalevelofabout6poundspermillion standardcubicfeet.Asreservoirpressuredeclines,thewatercontentincreasestoasmuchas threebarrelspermillionstandardcubicfeet.Sincethisadditionalcontenthascomefromvaporizationoftheconnatewater,itwouldappearthatanyfreshwaterproducedinexcessoftheinitial contentshouldbetreatedasproducedwaterandtakencareofintheWptermratherthantheGp term.Ifthewaterissaline,itdefinitelyisproducedwater;however,itincludesthefractionof abarrelpermillioncubicfeetobtainedfromthegasphase.Iftheproducedgasisbasedonthe dehydratedgasvolume,thegasvolumeshouldbeincreasedbythegasequivalentofthewater contentattheinitialreservoirpressureandtemperature,regardlessofthesubsequentdeclinein reservoir pressure, and the water production should be diminished by the water content.This amountstoabouta0.05%increaseintheproducedgasvolumes. 4.5 Gas Reservoirs as Storage Reservoirs Thedemandfornaturalgasisseasonal.Duringwintermonths,thereisamuchgreaterdemandfor naturalgasthanduringthewarmersummermonths.Tomeetthisvariabledemand,severalmeans ofstoringnaturalgasareusedintheindustry.Oneofthebestmethodsofstoringnaturalgasiswith theuseofdepletedgasreservoirs.Gasisinjectedduringthewarmsummermonthswhenthereis anoverabundanceandproducedduringthewintermonthswhenthereisashortageofsupply.Katz andTekhavepresentedagoodoverviewofthissubject.11 Katz and Tek listed three primary objectives in the design and operation of a gas storagereservoir:(1)verificationofinventory,(2)retentionagainstmigration,and(3)assuranceof Chapter 4 108 • Single-Phase Gas Reservoirs p/z deliverability.Verificationofinventorysimplymeansknowingthestoragecapacityofthereservoir asafunctionofpressure.Thissuggeststhatap/zplotorsomeothermeasureofmaterialbalancebe knownforthereservoirofinterest.Retentionagainstmigrationreferstoamonitoringsystemcapableofascertainingiftheinjectedgasremainsinthestoragereservoir.Obviously,leaksincasing andsoonwouldbedetrimentaltothestorageprocess.Theoperatorneedstobeassuredthatthe reservoircanbeproducedduringpeakdemandtimesinordertoprovidetheproperdeliverability. Amajorconcernwiththedeliverabilityisthatwaterencroachmentnotinterferewiththegasproduction.Withthesedesignconsiderationsinmind,itisapparentthatagoodcandidateforastorage reservoirwouldbeadepletedvolumetricgasreservoir.Withadepletedvolumetricreservoir,the p/zversusGpcurveisusuallyknownandwaterinfluxisnotaproblem. Ikokudefinesthreetypesofgasinvolvedinagasstoragereservoir.12Thefirstisthebasegas,or cushiongas,thatremainswhenthebasepressureisreached.Thebasepressureisthepressureatwhich production is stopped and injection begins.The second type of gas is the working gas, or working storage,thatisproducedandinjectedduringthecycleprocess.Thethirdtypeistheunusedgasthatessentiallyistheunusedcapacityofthereservoir.Figure4.5definesthesethreetypesofgasonap/zplot. The base pressure, and therefore the amount of base gas, is defined by deliverability needs.Sufficientpressuremustbemaintainedinthereservoirforreservoirgastobedelivered Unused gas 0 Working gas Base gas Gp 0 Figure 4.5 p/z plot showing different types of gas in a gas storage reservoir. 4.5 Gas Reservoirs as Storage Reservoirs 109 p/z to transporting pipelines. Economics dictates the pressure at which injection of gas during thesummermonthsends.Compressioncostsmustbebalancedwiththeprojectedsupplyand demandofthewintermonths.Intheory,foravolumetricreservoir,thecyclesofinjectionand productionsimplyrunupanddownthep/zversusGpcurvebetweenthepressurelimitsjust discussed. In certain applications, the use of the delta pressure concept may be advantageous.11The deltapressureisdefinedasthepressureatmaximumstorageminustheinitialreservoirpressure. Undertherightconditions,anamountofgaslargerthantheinitialgasinplacecanbeachieved. Thisagainisdictatedbytheeconomicsofthegivensituation. Hollispresentedaninterestingcasehistoryoftheconsiderationsinvolvedinchangingthe RoughGasFieldintheNorthSeaovertoastoragereservoir.13Considerationsinthedesignof storageanddeliverabilityratesincludedtheprobabilityofaseverewinteroccurringinthedemand area.Aseverewinterwasgivenaprobabilityof1in50.Hollisconcludedthatthedifferencesbetweenoffshoreandonshorestoragefacilitiesareduemainlytoeconomicfactorsandtheintegrated planningthatmusttakeplaceinoffshoredevelopment. Storageisausefulapplicationofgasreservoirs.Weencouragethereadertopursuethereferencesformoredetailedinformation,ifitbecomesnecessary. Gp Figure 4.6 p/z plot illustrating nonlinear behavior of abnormally pressured reservoir. 110 Chapter 4 • Single-Phase Gas Reservoirs 4.6 Abnormally Pressured Gas Reservoirs Normalpressuregradientsobservedingasreservoirsareintherangeof0.4to0.5psiperfootof depth.Reservoirswithabnormalpressuresmayhavegradientsashighas0.7to1.0psiperfootof depth.14,15,16,17Bernardhasreportedthatmorethan300gasreservoirshavebeendiscoveredinthe offshoreGulfCoastalone,withinitialgradientsinexcessof0.65psiperfootofdepthinformationsover10,000feetdeep.17 Whenthewaterandformationcompressibilityterminthematerialbalanceequationcanbe ignored,thenormalp/zbehaviorforavolumetricgasreservoirplotsastraightlineversuscumulativegasproduced(Fig.4.2).Thisisnotthecaseforanabnormallypressuredgasreservoir,ascan beseeninFig.4.6,whichillustratesthep/zbehaviorforthistypeofreservoir. Foranabnormallypressuredvolumetricreservoir,thep/zplotisastraightlineduringthe earlylifeofproduction,butthenitusuallycurvesdownwardduringthelaterstagesofproduction. IftheearlydataareusedtoextrapolateforGorforanabandonmentGp,theextrapolationcanyield significanterrors. Toexplainthecurvatureinthep/zplotforabnormallypressuredreservoirs,Harvilleand Hawkinspostulateda“rockcollapse”theorythatusedahighrockcompressibilityatabnormally high pressures and a reduced rock compressibility at normal reservoir pressures.14 However, workingwithrocksamplestakenfromabnormallypressuredreservoirs,Jogi,Gray,Ashman,and Thompson,andSinha,Holland,Borshcel,andSchatzreportedrockcompressibilitiesmeasured athighpressuresintheorderof2to5(10)–6 psi–1.18,19Thesevaluesarerepresentativeoftypical values at low pressures and suggest that rock compressibilities do not change with pressure. RamagostandFarshadshowedthatinsomecasesthep/zdatacouldbeadjustedtoyieldstraightlinebehaviorbyincludingthewaterandformationcompressibilityterm.20Bourgoyne,Hawkins, Lavaquial,andWickenhausersuggestedthatthenonlinearbehaviorcouldbeduetowaterinflux fromshales.21 Bernard has proposed a method of analyzing the p/z curve for abnormally pressured reservoirstodetermineinitialgasinplaceandgasreserveasafunctionofabandonmentp/z.17The methodusestwoapproaches.Thefirstinvolvestheearlyproductionlifewhenthep/zplotexhibits linearbehavior.Bernarddevelopedacorrelationforactualgasinplaceasafunctionofapparent gasinplace,asshowninFig.4.7. Theapparentgasinplaceisobtainedbyextrapolatingtheearly,linearp/zdata.Then,byenteringFig.4.7withtheapparentvalueofthegasinplace,theratioofactualgasinplacetoapparent gasinplacecanbeobtained.Thecorrelationappearstobereasonablyaccurateforthereservoirs Bernardstudied.Forlaterproductiontimes,whenthep/zdataexhibitnonlinearbehavior,Bernard definedaconstantC′accordingtoEq.(4.23), p p p (1 − C ′Δp) = i − i G p z zi zi G where (4.23) 4.6 Abnormally Pressured Gas Reservoirs 111 1.0 Actual gas in place/apparent gas in place 0.9 0.8 0.7 0.6 0.5 0.4 0 0 Figure 4.7 200 400 600 800 1000 Apparent gas in place, MMMCF 1200 1400 Correction for initial gas in place (after Bernard).17 C′=constant Δp=totalpressuredropinthereservoir,pi – p InEq.(4.23),theonlyunknownsareC′ and G.Bernardsuggeststheycanbefoundbythefollowingprocedure:First,calculateA′ and B′from p pi z − z i A' = Δp( p / z ) and pi z G p B' = i Δp( p / z ) Chapter 4 112 • Single-Phase Gas Reservoirs Iftherearendatapointsforp/z and Gp,thenC′ and Gcanbecalculatedfromthefollowing equations: G= ∑ B ' ∑ B '/ n − ∑ ( B '2 ) ∑ A ' B '− ∑ A ' ∑ B '/ n 1 C ' = ∑ A '/ n + ∑ B '/ n G 4.7 Limitations of Equations and Errors Theprecisionofthereservecalculationsbythevolumetricmethoddependsontheaccuracyofthe datathatenterthecomputations.Theprecisionoftheinitialgasinplacedependsontheprobable errorsintheaveragesoftheporosity,connatewater,pressure,andgasdeviationfactorandinthe errorinthedeterminationofthebulkproductivevolume.Withthebestofcoreandlogdatainratheruniformreservoirs,itisdoubtfulthattheinitialgasinplacecanbecalculatedmoreaccurately thanabout5%,andthefigurewillrangeupwardto100%orhigher,dependingontheuniformity ofthereservoirandthequantityandqualityofthedataavailable. Thereserveistheproductofthegasinplaceandtherecoveryfactor.Forvolumetricreservoirs,thereserveofthereservoirasawhole,foranyselectedabandonmentpressure,shouldbe knowntoaboutthesameprecisionastheinitialgasinplace.Water-drivereservoirsrequire,inaddition,theestimateofthevolumeofthereservoirinvadedatabandonmentandtheaverageresidual gassaturation.Whenthereservoirexhibitspermeabilitystratification,thedifficultiesareincreased andtheaccuracyisthereforereduced.Ingeneral,reservecalculationsaremoreaccurateforvolumetricthanforwater-drivereservoirs.Whenthereservesareplacedonawellorleasebasis,the accuracymaybereducedfurtherbecauseofleasedrainage,whichoccursinbothvolumetricand water-drivereservoirs. Theuseofthematerialbalanceequationtocalculategasinplaceinvolvesthetermsofthe gasvolumefactor.Theprecisionofthecalculationsis,ofcourse,afunctionoftheprobableerror intheseterms.TheerroringasproductionGparisesfromerroringasmetering,intheestimateof leaseuseandleakage,andintheestimateofthelow-pressureseparatororstock-tankgases.Sometimesundergroundleakageoccurs—fromthefailureincasingcementing,fromcasingcorrosion, or,inthecaseofdualcompletions,fromleakagebetweenthetwozones.Whengasiscommingled fromtworeservoirsatthesurfacepriortometering,thedivisionofthetotalbetweenthetworeservoirsdependsonperiodicwelltests,whichmayintroduceadditionalinaccuracies.Metersare usuallycalibratedtoanaccuracyof1%,and,therefore,itisdoubtfulthatthegasproductionunder thebestofcircumstancesisknowncloserthan2%.Averageaccuraciesareintherangeofafewto severalpercentagepoints. Pressureerrorsarearesultofgaugeerrorsandthedifficultiesinaveraging,particularlywhen therearelargepressuredifferencesthroughoutthereservoir.Whenreservoirpressuresareestimated frommeasuredwellheadpressures,theerrorsofthistechniqueenterthecalculations.Whenthefield isnotfullydeveloped,theaveragepressureis,ofcourse,takenfromthedevelopedportion,whichis Problems 113 lowerthanthatofthereservoirasawhole.Waterproductionwithgaswellsisfrequentlyunreported whentheamountissmall;whenitisappreciable,itisoftenestimatedfromperiodicwelltests. Underthebestofcircumstances,thematerialbalanceestimatesofthegasinplaceareseldom moreaccuratethan5%andmayrangemuchhigher.Theestimateofreservesis,ofcourse,onestep removed. Problems 4.1 Avolumetricgasfieldhasaninitialpressureof4200psia,aporosityof17.2%,andconnate waterof23%.Thegasvolumefactorat4200psiais0.003425ft3/SCFandat750psiais 0.01852ft3/SCF. (a) Calculatetheinitialin-placegasinstandardcubicfeetonaunitbasis. (b) Calculate the initial gas reserve in standard cubic feet on a unit basis, assuming an abandonmentpressureof750psia. (c) Explainwhythecalculatedinitialreservedependsontheabandonmentpressureselected. (d) Calculatetheinitialreserveofa640-acreunitwhoseaveragenetproductiveformation thicknessis34ft,assuminganabandonmentpressureof750psia. (e) Calculatetherecoveryfactorbasedonanabandonmentpressureof750psia. 4.2 Discoverywell1andwells2and4producegasinthe7500-ftreservoiroftheEchoLake Field (Fig. 4.8).Wells 3 and 7 were dry in the 7500-ft reservoir; however, together with their electric logs and the one from well 1, the fault that seals the northeast side of the 7 3 4 1 7500 7550 G/W 2 con tac 5 Figure 4.8 6 7600 t 7650 Echo Lake Field, subsurface map, 7500-ft reservoir. N Chapter 4 114 • Single-Phase Gas Reservoirs reservoirwasestablished.Thelogsofwells1,2,4,5,and6wereusedtoconstructthemapof Fig.4.8,whichwasusedtolocatethegas-watercontactanddeterminetheaveragenetsand thickness.Thereservoirhadbeenproducingfor18monthswhenwell6wasdrilledatthe gas-watercontact.Thestaticwellheadpressuresoftheproductionwellsshowedvirtuallyno declineduringthe18-monthperiodbeforedrillingwell6andaveragednear3400psia.The followingdatawereavailablefromelectriclogs,coreanalysis,andthelike: Averagewelldepth=7500ft Averagestaticwellheadpressure=3400psia Reservoirtemperature=175°F Gasspecificgravity=0.700 Averageporosity=27% Averageconnatewater=22% Standardconditions=14.7psiaand60°F Bulkvolumeofproductivereservoirrockatthetimewell6wasdrilled=22,500ac-ft (a) (b) (c) (d) (e) Calculatethereservoirpressure. Estimatethegasdeviationfactorandthegasvolumefactor. Calculatethereserveatthetimewell6wasdrilled,assumingaresidualgassaturationof30%. Discussthelocationofwell1withregardtotheoverallgasrecovery. Discuss the effect of sand uniformity on overall recovery—for example, a uniform permeablesandversusasandintwobedsofequalthickness,withrespectivepermeabilitiesof500mdand100md. 4.3 TheMSandisasmallgasreservoirwithaninitialbottom-holepressureof3200psiaand bottom-holetemperatureof220°F.Itisdesiredtoinventorythegasinplaceatthreeproductionintervals.Thepressure-productionhistoryandgasvolumefactorsareasfollows: Pressure (psia) Cumulative gas production (MM SCF) Gas Volume Factor (ft3/SCF) 3200 0 0.0052622 2925 79 0.0057004 2525 221 0.0065311 2125 452 0.0077360 (a) Calculatetheinitialgasinplaceusingproductiondataattheendofeachoftheproductionintervals,assumingvolumetricbehavior. (b) Explainwhythecalculationsofpart(a)indicateawaterdrive. (c) Showthatawaterdriveexistsbyplottingthecumulativeproductionversusp/z. (d) Basedonelectriclogandcoredata,volumetriccalculationsontheMSandshowedthat Problems 115 theinitialvolumeofgasinplaceis1018MMSCF.Ifthesandisunderapartialwater drive,whatisthevolumeofwaterencroachedattheendofeachoftheperiods?There wasnoappreciablewaterproduction. 4.4 WhentheSabineGasFieldwasbroughtin,ithadareservoirpressureof1700psiaanda temperatureof160°F.After5.00MMMSCFwasproduced,thepressurefellto1550psia. Ifthereservoirisassumedtobeundervolumetriccontrol,usingthedeviationfactorsof Problem2.10,calculatethefollowing: (a) Thehydrocarbonporevolumeofthereservoir. (b) TheSCFproducedwhenthepressurefallsto1550,1400,1100,500,and200psia.Plot cumulativerecoveryinSCFversusp/z. (c) TheSCFofgasinitiallyinplace. (d) Fromyourgraph,findhowmuchgascanbeobtainedwithouttheuseofcompressors fordeliveryintoapipelineoperatingat750psia. (e) WhatistheapproximatepressuredropperMMMSCFofproduction? (f) Calculatetheminimumvalueoftheinitialreserveiftheproducedgasmeasurementis accurateto±5%andiftheaveragepressuresareaccurateto±12psiwhen5.00MMM SCFhavebeenproducedandthereservoirpressurehasdroppedto1550psia. 4.5 If, however, during the production of 5.00 MMM SCF of gas in the preceding problem, 4.00MMbblofwaterencroachesintothereservoirandstillthepressurehasdroppedto 1550psia,calculatetheinitialin-placegas.HowdoesthiscomparewithProblem4.4(c)? 4.6 (a) T hegascapoftheSt.JohnOilFieldhadabulkvolumeof17,000ac-ftwhenthereservoir pressurehaddeclinedto634psig.Coreanalysisshowsanaverageporosityof18%andan averageinterstitialwaterof24%.Itisdesiredtoincreasetherecoveryofoilfromthefield byrepressuringthegascapto1100psig.Assumingthatnoadditionalgasdissolvesinthe oilduringrepressuring,calculatetheSCFrequired.Thedeviationfactorsforboththereservoirgasandtheinjectedgasare0.86at634psigand0.78at1100psig,bothat130°F. (b) Iftheinjectedgashasadeviationfactorof0.94at634psigand0.88at1100psigand thereservoirgasdeviationfactorsmatchthosepresentedin(a),recalculatetheinjected gasrequired. (c) Istheassumptionthatnoadditionalsolutiongaswillenterthereservoiroilavalidone? (d) Considering the possibility of some additional solution gas and the production of oil duringthetimeofinjection,willthefigureofpart(a)bemaximumorminimum?Explain. (e) Explainwhythegasdeviationfactorsarehigher(closertounity)fortheinjectedgasin part(b)thanforthereservoirgas. 4.7 Thefollowingproductiondataareavailablefromagasreservoirproducedundervolumetric control: Chapter 4 116 • Single-Phase Gas Reservoirs Pressure (psia) Cumulative gas production (MMM SCF) 5000 200 4000 420 Theinitialreservoirtemperaturewas237°F,andthereservoirgasgravityis0.7. (a) Whatwillbethecumulativegasproductionat2500psia? (b) Whatfractionoftheinitialreservoirgaswillbeproducedat2500psia? (c) Whatwastheinitialreservoirpressure? 4.8 (a) A welldrilledintoagascapforgasrecyclingpurposesisfoundtobeinanisolatedfaultblock.After50MMSCFwasinjected,thepressureincreasedfrom2500to 3500psia.Deviationfactorsforthegasare0.90at3500and0.80at2500psia,andthe bottom-holetemperatureis160°F.Howmanycubicfeetofgasstoragespaceareinthe faultblock? (b) Iftheaverageporosityis16%,averageconnatewateris24%,andaveragesandthicknessis12ft,whatisthearealextentofthefaultblock? 4.9 TheinitialvolumeofgasinplaceinthePSandreservoiroftheHoldenFieldiscalculated fromelectriclogandcoredatatobe200MMMSCFunderlying2250productiveacres,at aninitialpressureof3500psiaand140°F.Thepressure-productionhistoryis Pressure (psia) Production (MMM SCF) Gas deviation factor at 140°F 3500(initial) 0.0 0.85 2500 75.0 0.82 (a) Whatistheinitialvolumeofgasinplaceascalculatedfromthepressure-production history,assumingnowaterinflux? (b) Assuminguniformsandthickness,porosity,andconnatewater,ifthevolumeofgas inplacefrompressure-productiondataisbelievedtobecorrect,howmanyacresof extensiontothepresentlimitsofthePSandarepredicted? (c) If,ontheotherhand,thegasinplacecalculatedfromthelogandcoredataisbelieved tobecorrect,howmuchwaterinfluxmusthaveoccurredduringthe75MMMSCFof productiontomakethetwofiguresagree? 4.10 Explainwhyinitialcalculationsofgasinplacearelikelytobeingreatererrorduringtheearly lifeofdepletionreservoirs.Willthesefactorsmakethepredictionshighorlow?Explain. 4.11 Agasreservoirunderpartialwaterdriveproduced12.0MMMSCFwhentheaveragereservoirpressuredroppedfrom3000psiato2200psia.Duringthesameinterval,anestimated Problems 117 5.20 MM bbl of water entered the reservoir based on the volume of the invaded area. If thegasdeviationfactorat3000psiaandbottom-holetemperatureof170°Fis0.88andat 2200psiais0.78,whatistheinitialvolumeofgasinplacemeasuredat14.7psiaand60°F? 4.12 Agas-producingformationhasuniformthicknessof32ft,aporosityof19%,andconnate watersaturationof26%.Thegasdeviationfactoris0.83attheinitialreservoirpressureof 4450psiaandreservoirtemperatureof175°F. (a) Calculatetheinitialin-placegasperacre-footofbulkreservoirrock. (b) Howmanyyearswillittakeawelltodepleteby50%a640-acreunitattherateof 3MMSCF/day? (c) Ifthereservoirisunderanactivewaterdrivesothatthedeclineinreservoirpressure is negligible and, during the production of 50.4 MMM SCF of gas, water invades 1280acres,whatisthepercentageofrecoverybywaterdrive? (d) Whatisthegassaturationasapercentageoftotalporespaceintheportionofthe reservoirinvadedbywater? 4.13 Fiftybillionstandardcubicfeetofgashasbeenproducedfromadrygasreservoirsince itsdiscovery.Thereservoirpressureduringthisproductionhasdroppedto3600psia.Your company,whichoperatesthefield,hascontractedtousethereservoirasagasstoragereservoir.A gas with a gravity of 0.75 is to be injected until the average pressure reaches 4800psia.Assumethatthereservoirbehavesvolumetrically,anddeterminetheamountof SCFofgasthatmustbeinjectedtoraisethereservoirpressurefrom3600to4800psia.The initialpressureandtemperatureofthereservoirwere6200psiaand280°F,respectively,and thespecificgravityofthereservoirgasis0.75. 4.14 Theproductiondataforagasfieldaregiveninthefollowingtable.Assumevolumetricbehaviorandcalculatethefollowing: (a) Determinetheinitialgasinplace. (b) Whatpercentageoftheinitialgasinplacewillberecoveredatp/zof1000? (c) The field is to be used as a gas storage reservoir into which gas is injected during summermonthsandproducedduringthepeakdemandmonthsofthewinter.Whatis theminimump/zvaluethatthereservoirneedstobebroughtbackuptoifasupplyof 50MMMSCFofgasisrequiredandtheabandonmentp/zis1000? p /z (psia) Gp (MMM SCF) 6553 0.393 6468 1.642 6393 3.226 (continued) Chapter 4 118 • Single-Phase Gas Reservoirs p/z (psia) Gp (MMM SCF) 6329 4.260 6246 5.504 6136 7.538 6080 8.749 4.15 Calculatethedailygasproduction,includingthecondensateandwatergasequivalents,for areservoirwiththefollowingdailyproduction: Separatorgasproduction=6MMSCF Condensateproduction=100STB Stock-tankgasproduction=21MSCF Freshwaterproduction=10surfacebbl Initialreservoirpressure=6000psia Currentreservoirpressure=2000psia Reservoirtemperature=225°F Watervaporcontentof6000psiaand225°F=0.86bbl/MMSCF Condensategravity=50°API References 1. 2. 3. 4. 5. 6. 7. 8. 9. HaroldVance,Elements of Petroleum Subsurface Engineering,EducationalPublishers,1950. L.W.LeRoy,Subsurface Geologic Methods,2nded.,ColoradoSchoolofMines,1950. M.Shepherd,“Volumetrics,”Oil Field Production Geology: AAPG Memoir 91(2009),189–93. H.H.Kaveler,“EngineeringFeaturesoftheSchulerFieldandUnitOperation,”Trans.AlME (1944),155,73. T.M.Geffen,D.R.Parrish,G.W.Haynes,andR.A.Morse,“EfficiencyofGasDisplacement fromPorousMediabyLiquidFlooding,”Trans.AlME(1952),195,37. R.Agarwal,R.Al-Hussainy,andH.J.Ramey,“TheImportanceofWaterInfluxinGasReservoirs,”Jour. of Petroleum Technology(Nov.1965),1336–42. G.Matthes,R.F.Jackson,S.Schuler,andO.P.Marudiak,“ReservoirEvaluationandDeliverabilityStudy,BierwangField,WestGermany,”Jour. of Petroleum Technology(Jan.1973),23. T.L.Lutes,C.P.Chiang,M.M.Brady,andR.H.Rossen,“AcceleratedBlowdownofaStrong WaterDriveGasReservoir,”paperSPE6166,presentedatthe51stAnnualFallMeetingofthe SocietyofPetroleumEngineersofAlME,Oct.3–6,1976,NewOrleans,LA. D.P.ArcanoandZ.Bassiouni,“TheTechnicalandEconomicFeasibilityofEnhancedGas RecoveryintheEugeneIslandFieldbyUseoftheCoproductionTechnique,”Jour. of Petroleum Technology(May1987),585. References 119 10. EugeneL.McCarthy,WilliamL.Boyd,andLawrenceS.Reid,“TheWaterVaporContentof Essentially Nitrogen-Free Natural Gas Saturated atVarious Conditions ofTemperature and Pressure,”Trans.AlME(1950),189,241–42. 11. D.I.KatzandM.R.Tek,“OverviewonUndergroundStorageofNaturalGas,”Jour. of Petroleum Technology(June1981),943. 12. ChiU.Ikoku,Natural Gas Reservoir Engineering,Wiley,1984. 13. A.P.Hollis,“SomePetroleumEngineeringConsiderationsintheChangeoveroftheRough GasFieldtotheStorageMode,”Jour. of Petroleum Technology(May1984),797. 14. D.W.HarvilleandM.F.HawkinsJr.,“RockCompressibilityandFailureasReservoirMechanismsinGeopressuredGasReservoirs,”Jour. of Petroleum Technology(Dec.1969),1528–30. 15. I.Fatt,“CompressibilityofSandstonesatLowtoModeratePressures,”AAPG Bull.(1954), No.8,1924. 16. J.O.Duggan,“TheAnderson‘L’—AnAbnormallyPressuredGasReservoirinSouthTexas,” Jour. of Petroleum Technology(Feb.1972),132. 17. W. J. Bernard, “Reserves Estimation and Performance Prediction for Geopressured Reservoirs,”Jour. of Petroleum Science and Engineering(1987),1,15. 18. P.N.Jogi,K.E.Gray,T.R.Ashman,andT.W.Thompson,“CompactionMeasurementsof Cores from the Pleasant Bayou Wells,” presented at the 5th Conference on GeopressuredGeothermalEnergy,Oct.13–15,1981,BatonRouge,LA. 19. K.P.Sinha,M.T.Holland,T.F.Borschel,andJ.P.Schatz,“MechanicalandGeologicalCharacteristicsofRockSamplesfromSweezyNo.1WellatParcperdueGeopressured/Geothermal Site,”reportofTerraTek,Inc.toDowChemicalCo.,USDepartmentofEnergy,1981. 20. B. P. Ramagost and F. F. Farshad, “P/ZAbnormally Pressured Gas Reservoirs,” paper SPE 10125,presentedattheAnnualFallMeetingofSPEofAlME,Oct.5–7,1981,SanAntonio,TX. 21. A.T.Bourgoyne,M.F.Hawkins,F.P.Lavaquial,andT.L.Wickenhauser,“ShaleWaterasa PressureSupportMechanisminSuperpressureReservoirs,”paperSPE3851,presentedatthe ThirdSymposiumAbnormalSubsurfacePorePressure,May1972,BatonRouge,LA. This page intentionally left blank C H A P T E R 5 Gas-Condensate Reservoirs 5.1 Introduction Gas-condensateproductionmaybethoughtofasintermediatebetweenoilandgas.Oilreservoirs haveadissolvedgascontentintherangeofzero(deadoil)toafewthousandcubicfeetperbarrel, whereasingasreservoirs,1bblofliquid(condensate)isvaporizedin100,000SCFofgasormore, fromwhichasmallornegligibleamountofhydrocarbonliquidisobtainedinsurfaceseparators. Gas-condensateproductionispredominantlygasfromwhichmoreorlessliquidiscondensed in thesurfaceseparators—hencethenamegas condensate.Theliquidissometimescalledbyanoldername,distillate,andalsosometimessimplyoilbecauseitisanoil.Gas-condensatereservoirs maybeapproximatelydefinedasthosethatproducelight-coloredorcolorlessstock-tankliquids withgravitiesabove45°APIatgas-oilratiosintherangeof5000to100,000SCF/STB.Allenhas pointedouttheinadequacyofclassifyingwellsandthereservoirsfromwhichtheyproduceentirely onthebasisofsurfacegas-oilratios—fortheclassificationofreservoirs,asdiscussedinChapter1, properlydependson(1)thecompositionofthehydrocarbonaccumulationand(2)thetemperature andpressureoftheaccumulationintheEarth.1 Asthesearchfornewfieldsledtodeeperdrilling,newdiscoveriesconsistedpredominately of gas and gas-condensate reservoirs. Figure 5.1, based on well test data reported in Ira Rinehart’s Yearbooks,showsthediscoverytrendfor17parishesinsouthwestLouisianafor1952–56, inclusive.2Thereservoirswereseparatedintooilandgasorgas-condensatetypesonthebasisof welltestgas-oilratiosandtheAPIgravityoftheproducedliquid.Oildiscoveriespredominated atdepthslessthan8000ft,butgasandgas-condensatediscoveriespredominatedbelow10,000ft. Thedeclineindiscoveriesbelow12,000ftwasduetothefewernumberofwellsdrilledbelowthat depthratherthantoadropintheoccurrenceofhydrocarbons.Figure5.2showsthesamedatafor theyear1955withthegas-oilratioplottedversusdepth.Thedashedlinemarked“oil”indicatesthe generaltrendtoincreasedsolutiongasinoilwithincreasingpressure(depth),andtheenvelopto thelowerrightenclosesthosediscoveriesthatwereofthegasorgas-condensatetypes. Muskat, Standing, Thornton, and Eilerts have discussed the properties and behavior of gas-condensate reservoirs.3–6Table 5.1, taken from Eilerts, shows the distribution of the gas-oil 121 Chapter 5 122 • Gas-Condensate Reservoirs 3 5 Oil Depth, thousands of ft 7 9 11 13 Gas condensate and gas 15 17 0 10 20 30 Number of discovers per 1000-ft interval 40 Figure 5.1 Discovery frequency of oil and gas or gas-condensate reservoirs versus depth for 17 parishes in southwest Louisiana, 1952–56, inclusive (data from Ira Rinehart’s Yearbooks).2 ratioandtheAPIgravityamong172gasandgas-condensatefieldsinTexas,Louisiana,andMississippi.6Theseauthorsfoundnocorrelationbetweenthegas-oilratioandtheAPIgravityofthe tankliquidforthesefields. Inagas-condensatereservoir,theinitialphaseisgas,buttypicallythefluidofcommercialinterestisthegascondensate.Thestrategiesformaximizingrecoveryofthecondensate distinguishgas-condensatereservoirsfromsingle-phasegasreservoirs.Forexample,inasingle-phase gas reservoir, reducing the reservoir pressure increases the recovery factor, and a waterdriveislikelytoreducetherecoveryfactor.Inagas-condensatereservoir,reducingthe 5.1 Introduction 123 3 5 Depth, thousands of ft 7 Oil 9 11 Gas condensate and gas 13 15 17 100 Figure 5.2 1000 10,000 Gas-oil ratio, SCF/STB 100,000 Plot showing trend of increase of gas-oil ratio versus depth for 17 parishes in southwest Louisiana during 1955 (data from Ira Rinehart’s Yearbooks).2 reservoirpressurebelowthedew-pointpressurereducescondensaterecovery,andthereforea waterdrivethatmaintainsthereservoirpressureabovethedew-pointpressurewilllikelyincreasecondensaterecovery.Similarly,strategiesforincreasingcondensaterecoverydifferfrom thoseusedforoilrecovery.Inparticular,injectingwatermaintainspressureanddisplacesoil towardproducingwells,butforcondensate,itisbettertousegasasapressuremaintenance anddisplacementfluid.Thischapterwillaidtheengineerindesigningarecoveryplanfora gas-condensate reservoir that will attempt to maximize the production of the more valuable componentsofthereservoirfluid. Chapter 5 124 Table 5.1 • Gas-Condensate Reservoirs Range of Gas-Oil Ratios and Tank Oil Gravities for 172 Gas and Gas-Condensate Fields in Texas, Louisiana, and Mississippi Number of fields Total Percent of total 7 57 33.1 18 4 55 32.0 12 15 5 32 18.6 26.2to35.0 1 8 1 10 5.8 21.0to26.2 1 3 1 5 2.9 <21.0 2 5 6 13 7.6 87 61 24 172 100 Range of gas-oil ratio (M SCF/STB) Texas Louisiana Mississippi >105 38 12 0.4to0.8 52.5to105 33 0.8to1.2 35.0to52.5 1.2to1.6 1.6to2.0 Range of liquid-gas ratio (GPM)a <0.4 >2.0 Total Range of stock-tank gravity (°API) a <40 2 1 0 3 1.8 40–45 4 2 0 6 3.6 45–50 12 12 0 24 14.6 50–55 23 17 7 47 28.5 55–60 24 13 12 49 29.7 60–65 19 8 3 30 18.2 >65 3 1 2 6 3.6 87 54 24 165 100 Gallonsper1000SCF 5.2 Calculating Initial Gas and Oil Theinitialgasandoil(condensate)forgas-condensatereservoirs,bothretrogradeandnonretrograde,maybecalculatedfromgenerallyavailablefielddatabyrecombiningtheproducedgasand oilinthecorrectratiotofindtheaveragespecificgravity(air=1.00)ofthetotalwellfluid,whichis presumablybeingproducedinitiallyfromaone-phasereservoir.Considerthetwo-stageseparation systemshowninFig.1.3.TheaveragespecificgravityofthetotalwellfluidisgivenbyEq.(5.1): γw = R1γ 1 + 4602γ o + R3γ 3 133,316γ o + R3 R1 + M wo where R1, R3=producinggas-oilratiosfromtheseparator(1)andstocktank(3) γ1, γ3=specificgravitiesofseparatorandstock-tankgases γo=specificgravityofthestock-tankoil(water=1.00),givenby (5.1) 5.2 Calculating Initial Gas and Oil 125 γo = 141.5 ρo,API + 131.5 (5.2) Mwo=molecularweightofthestock-tankoilthatisgivenbyEq.(4.20): M wo = 5954 42.43γ o = ρo,API − 8.811 1.008 − γ o (4.20) Example5.1showstheuseofEq.(5.1)tocalculatetheinitialgasandoilinplaceperacre-foot ofagas-condensatereservoirfromtheusualproductiondata.Thethreeexampleproblemsinthis chapterrepresentthetypeofcalculationsthatanengineerwouldperformondatageneratedfrom laboratorytestsonreservoirfluidsamplesfromgas-condensatesystems.Samplereportscontaining additionalexamplecalculationsmaybeobtainedfromcommerciallaboratoriesthatconductPVT studies.Theengineerdealingwithgas-condensatereservoirsshouldobtainthesesamplereports tosupplementthematerialinthischapter.Thegasdeviationfactoratinitialreservoirtemperature andpressureisestimatedfromthegasgravityoftherecombinedoilandgas,asshowninChapter 2.Fromtheestimatedgasdeviationfactorandthereservoirtemperature,pressure,porosity,and connatewater,themolesofhydrocarbonsperacre-footcanbecalculated,andfromthis,theinitial gasandoilinplace. Example 5.1 Calculating the Initial Oil and Gas in Place per Acre-Foot for a Gas-Condensate Reservoir Given Initialpressure=2740psia Reservoirtemperature=215°F Averageporosity=25% Averageconnatewater=30% Dailytankoil=242STB Oilgravity,60°F=48.0°API Dailyseparatorgas=3100MCF Separatorgasspecificgravity=0.650 Dailytankgas=120MCF Tankgasspecificgravity=1.20 Solution γo = M wo = 141.5 = 0.788 48.0 + 131.5 5954 5954 = = 151.9 ρo,API − 8.811 48.0 − 8.811 Chapter 5 126 R1 = Gas-Condensate Reservoirs 3, 100, 000 = 12, 810 242 R3 = γw = • 120,000 = 496 242 12, 180(0.650 ) + 4602(0.788 ) + 496(1.20 ) = 0.896 133, 316(0.788 ) 12, 810 + + 496 151.9 FromEqs.(2.11)and(2.12),pc=636psiaand Tc = 430°R.Also,Tr=1.57andpr=4.30,from which,usingFig.2.2,thegasdeviationfactoris0.815attheinitialconditions.Thusthetotal initialgasinplaceperacre-footofbulkreservoiris G= 379.4 pV 379.4 (2740 )( 43560 )(0.25 )(1 − 0.30 ) = = 1342 MCF/ac-ft zR ' T 0.815(10.73)(675 ) Becausethevolumefractionequalsthemolefractioninthegasstate,thefractionofthetotal producedonthesurfaceasgasis R1 R3 + 379 . 4 379 .4 = fg = R1 R3 350γ o ng + no + + 379.4 379.4 M wo ng (5.3) 12, 810 496 + 379.4 379.4 fg = = 0.951 12, 810 496 350(0.788 ) + + 379.4 379.4 151.9 Thus Initialgasinplace=0.951(1342)=1276MCF/ac-ft Initialoilinplace = 1276(10 3 ) = 95.9 ST TB/ac-ft 12, 810 + 496 Becausethegasproductionis95.1%ofthetotalmolesproduced,thetotaldailygas-condensate productioninMCFis ΔG p = daily gas 3100 + 120 = = 3386 MCF/day 0.951 0.951 5.2 Calculating Initial Gas and Oil 127 Thetotaldailyreservoirvoidagebythegaslawis V = 3, 386, 000 675(14.7 )(0.815 ) = 19, 220 ft 3 /day 520(2740 ) 1400 Pseudocritical temperature, ºR 0 60/6 vity a r g ific Spec 0.95 0.90 1300 0.85 1200 0.80 0.75 1100 0.70 Pseudocritical pressure, psia 1000 500 400 0.70 0.75 0.80 0.85 0.95 0.90 Spec ific g ravit y 60 /60 300 200 Figure 5.3 100 120 140 160 180 Molecular weight 200 220 240 Correlation charts for estimation of the pseudocritical temperature and pressure of heptanes plus fractions from molecular weight and specific gravity (after Mathews, Roland, and Katz, proc. NGAA). 7 Chapter 5 128 • Gas-Condensate Reservoirs Thegasdeviationfactorofthetotalwellfluidatreservoirtemperatureandpressurecanalsobe calculatedfromitscomposition.Thecompositionofthetotalwellfluidiscalculatedfromtheanalyses oftheproducedgas(es)andliquidbyrecombiningthemintheratioinwhichtheyareproduced.When thecompositionofthestock-tankliquidisknown,aunitofthisliquidmustbecombinedwiththeproper amountsofgas(es)fromtheseparator(s)andthestocktank,eachofwhichhasitsowncomposition. When the compositions of the gas and liquid in the first or high-pressure separator are known, the shrinkagetheseparatorliquidundergoesinpassingtothestocktankmustbemeasuredorcalculated inordertoknowtheproperproportionsinwhichtheseparatorgasandliquidmustbecombined.For example,ifthevolumefactoroftheseparatorliquidis1.20separatorbblperstock-tankbarrelandthe measuredgas-oilratiois20,000SCFofhigh-pressuregasperbblofstock-tankliquid,thentheseparator gasandliquidsamplesshouldberecombinedintheproportionsof20,000SCFofgasto1.20bblof separatorliquid,since1.20bblofseparatorliquidshrinksto1.00bblinthestocktank. Example5.2showsthecalculationofinitialgasandoilinplaceforagas-condensatereservoirfromtheanalysesofthehigh-pressuregasandliquid,assumingthewellfluidtobethesame asthereservoirfluid.ThecalculationisthesameasthatshowninExample5.1,exceptthatthegas deviationfactorofthereservoirfluidisfoundfromthepseudoreducedtemperatureandpressure, which are determined from the composition of the total well fluid rather than from its specific Table 5.2 Calculations for Example 5.2 on Gas-Condensate Fluid (1) (2) (3) (4) Mole composition of separator fluids (5) (6) (7) (8) (3) × (4) lb/mol Liquid bbl/mol for each component (3) × (6) bbl of each component per mole of separator liquid Moles of each component in 59.11 moles of gas (2) × 59.11 Gas Liquid CO2 0.012 0 C1 0.9404 0.2024 16.04 3.2465 0.1317 0.0267 55.587 C2 0.0305 0.0484 30.07 1.4554 0.1771 0.0086 1.8029 C3 0.0095 0.0312 44.09 1.3756 0.248 0.0077 0.5615 iC4 0.0024 0.0113 58.12 0.6568 0.2948 0.0033 0.1419 nC4 0.0023 0.0196 58.12 1.1392 0.284 0.0056 0.136 Molecular weight 0.7093 iC5 0.0006 0.0159 72.15 1.1472 0.3298 0.0052 0.0355 nC5 0.0003 0.017 72.15 1.2266 0.3264 0.0055 0.0177 C6 0.0013 0.0384 86.17 3.3089 0.3706 0.0142 0.0768 + 7 C 0.0007 0.6158 185 113.923 0.6336 0.3902 0.0414 Total 1.0000 1.0000 0.4671 59.1100 127.4791 a 185lb/mol÷(0.8343×350lb/bbl)=0.6336bbl/mol b FromFig.5.3,afterMathews,Roland,andKatz,formolecularweightC7+=185andspecificgravity=0.83427 a 5.2 Calculating Initial Gas and Oil 129 gravity.Figure5.3presentschartsforestimatingthepseudocriticaltemperatureandpressureofthe heptanes-plusfractionfromitsmolecularweightandspecificgravity. Example 5.2 Calculating the Initial Gas and Oil in Place from the Compositions of the Gas and Liquid from the High-Pressure Separator Given Reservoirpressure=4350psia Reservoirtemperature=217°F Hydrocarbonporosity=17.4% Standardconditions=15.025psia,60°F Separatorgas=842,600SCF/day Stock-tankoil=31.1STB/day MolecularweightC7+inseparatorliquid=185.0 SpecificgravityC7+inseparatorliquid=0.8343 Specificgravityseparatorliquidat880psigand60°F=0.7675 Separatorliquidvolumefactor=1.235bbl/STBat880psia,bothat60°F (9) (10) (11) Mole Moles Moles of composiof each each comcomponent tion of total ponent well fluid in 61.217 in 2.107 mols of gas (10) ÷ 61.217 mols of and liquid liquid (8) + (9) (3) × 2.107 (12) (13) (14) (15) Critical pressure, psia Partial critical pressure, psia (11) × (12) Critical temp., °R Partial critical temperature, °R (11) × (14) 0.0000 0.7093 0.0116 1070 12.3981 548 6.3497 0.4265 56.0135 0.9150 673 615.7944 343 313.8447 0.1020 1.9050 0.0311 708 22.0321 550 17.1153 0.0657 0.6277 0.0103 617 6.3265 666 6.8290 0.0238 0.1658 0.0027 529 1.4327 735 1.9907 0.0413 0.1773 0.0029 550 1.5929 766 2.2185 0.0335 0.0685 0.0011 484 0.5416 830 0.9287 0.0358 0.0538 0.0009 490 0.4306 846 0.7435 0.0809 0.1579 0.0026 440 1.1349 914 1.2975 1.3385 0.0219 300 6.5595 1227 2.1070 61.2170 1.0000 b 668.2434 2.3575 b 26.8282 379.2058 Chapter 5 130 • Gas-Condensate Reservoirs Compositionsofhigh-pressuregasandliquid=Table5.2,columns2and3 Molarvolumeat15.025psiaand60°F=371.2ft3/mol Solution NotethatcolumnnumbersrefertoTable5.2: 1. Columns1,2,and3aregiven.Thisinformationtypicallycomesfromalabtestperformedonasampletakenfromtheseparator.Column4isadditionalinformationthat canalsobefoundinTable2.1.Usingthisinformation,calculatethemoleproportions inwhichtorecombinetheseparatorgasandliquid.Multiplythemolefractionofeach componentintheliquid(column3)byitsmolecularweight(column4)andenterthe productsincolumn5.Thesumofcolumn5isthemolecularweightoftheseparatorliquid,127.48.Next,theratioofliquidbarrelpermoleisneededforeachcomponent.This informationisalsofoundinTable2.1.ThelastcolumnofTable2.1istheestimated gal/lb-mol—thesedatawillneedtobeconvertedtobbl/mol.Thenextseveralstepsare usedtomatchthequantityofproducedliquidtoproducedgasanddeterminethecompositionoftheentirewellfluidratherthanjusttheliquidorgas.Becausethespecific gravityoftheseparatorliquidis0.7675at880psigand60°F,themolesperbarrelis 0.7675 × 350 lb/bbl = 2.107 moles/bblfor theseparator liquid 127.48 lb/mole Theseparatorliquidrateis31.1STB/day×1.235sep.bbl/STBsothattheseparatorgasoilratiois 842, 600 = 21, 940 SCFsep. gas/bblsep. lliquid 31.1 × 1.235 Becausethe21,940SCFis21,940/371.2,or59.11mols,theseparatorgasand liquidmustberecombinedintheratioof59.11molsofgasto2.107molsofliquid. Ifthespecificgravityoftheseparatorliquidisnotavailable,themoleperbarrel figuremaybecalculatedasfollows.Multiplythemolefractionofeachcomponentinthe liquid,column3,byitsbarrelpermolefigure,column6,obtainedfromdatain Table2.1,andentertheproductincolumn7.Thesumofcolumn7,0.46706,isthenumberofbarrelsofseparatorliquidpermoleofseparatorliquid,andthereciprocalis2.141 mols/bbl(versus2.107measured). 2. Nowthattheratioofthegastoliquidproducedisknown,recombine59.11molsofgas and2.107molsofliquid.Multiplythemolefractionofeachcomponentinthegas,column2,by59.11mols,andenterincolumn8.Multiplythemolefractionofeachcomponentintheliquid,column3,by2.107mols,andenterthesolutionincolumn9.Enterthe sumofthemolesofeachcomponentinthegasandliquid,column8,pluscolumn9,in column10.Divideeachfigureincolumn10bythesumofcolumn10,61.217,andenter 5.3 The Performance of Volumetric Reservoirs 131 thequotientsincolumn11,whichisthemolecompositionofthetotalwellfluid.Column 12isthecriticalpressureforeachcomponent;itisalsofoundinTable2.1.Withthat information,thepartialcriticalpressure(column13)canbefound.Thesamewillbedone forcolumns14and15fortemperature.Calculatethepseudocriticaltemperature379.23°R andpressure668.23psiafromthecompositionbysummingthepartialtemperatureand partialpressurevaluesforeachcomponent.Fromthepseudocriticals,findthepseudoreducedcriticalsandthenthedeviationfactorat4350psiaand217°F,whichis0.963. 3. Findthegasandoil(condensate)inplaceperacre-footofnetreservoirrock.Fromthe gaslaw,theinitialmolesperacre-footat17.4%hydrocarbonporosityis pV 4350 × ( 43, 560 × 0.174 ) = = 4713mools/ac-ft zRT 0.963 × 10.73 × 677 Gasmolefraction = Initialgasinplace = 59.11 = 0.966 59.11 + 2.107 0.966 × 4713 × 371.2 = 1690 MCF/ac-ft 1000 Initialoilinplace = (1 − 0.966 ) × 4713 = 661.6 STB/ac-ft 2.107 × 1.235 Becausethehigh-pressuregasis96.6%ofthetotalmoleproduction,thedailygascondensateproductionexpressedinstandardcubicfeetis ΔG p = Daily separator gas 842, 600 = = 872, 200 SCF/day Gasmolefraction 0.966 Thedailyreservoirvoidageat4350psiais ΔV = 872, 200 × 5.3 677 15.025 × × 0.963 = 3777 ft 3 /day 520 4350 The Performance of Volumetric Reservoirs Thebehaviorofsingle-phasegasreservoirsistreatedinChapter4.Sincenoliquidphasedevelopswithinthereservoir,wherethetemperatureisabovethecricondentherm,thecalculationsare simplified.Whenthereservoirtemperatureisbelowthecricondentherm,however,aliquidphase develops within the reservoir when pressure declines below the dew point, owing to retrograde condensation,andthetreatmentisconsiderablymorecomplex,evenforvolumetricreservoirs. Onesolutionistocloselyduplicatethereservoirdepletionbylaboratorystudiesonarepresentativesampleoftheinitial,single-phasereservoirfluid.Thesampleisplacedinahigh-pressure 132 Chapter 5 • Gas-Condensate Reservoirs cellatreservoirtemperatureandinitialreservoirpressure.Duringthedepletion,thevolumeofthe cellisheldconstanttoduplicateavolumetricreservoir,andcareistakentoremoveonlygas-phase hydrocarbons from the cell because, for most reservoirs, the retrograde condensate liquid that formsistrappedasanimmobileliquidphasewithintheporespacesofthereservoir. Laboratoryexperimentshaveshownthat,withmostrocks,theoilphaseisessentiallyimmobileuntilitbuildsuptoasaturationintherangeof10%to20%oftheporespace,dependingonthe natureoftherockporespacesandtheconnatewater.Becausetheliquidsaturationsformostretrogradefluidsseldomexceed10%,thisisareasonableassumptionformostretrogradecondensate reservoirs.Inthissameconnection,itshouldbepointedoutthat,inthevicinityofthewellbore, retrogradeliquidsaturationsoftenbuilduptohighervaluessothatthereistwo-phaseflow,bothgas andretrogradeliquid.Thisbuildupofliquidoccursastheone-phasegassuffersapressuredropas itapproachesthewellbore.Continuedflowincreasestheretrogradeliquidsaturationuntilthereis liquidflow.Althoughthisphenomenondoesnotaffecttheoverallperformanceseriouslyorenter intothepresentperformancepredictions,itcan(1)reduce,sometimesseriously,theflowrateof gas-condensatewellsand(2)affecttheaccuracyofwellsamplestaken,assumingone-phaseflow intothewellbore. Thecontinuousdepletionofthegasphase(only)ofthecellatconstantvolumecanbeclosely duplicatedbythefollowingmoreconvenienttechnique.Thecontentofthecellisexpandedfrom theinitialvolumetoalargervolumeatapressureafewhundredpsibelowtheinitialpressureby withdrawingmercuryfromthebottomofthecellorotherwiseincreasingthevolume.Timeisallowedforequilibriumtobeestablishedbetweenthegasphaseandtheretrogradeliquidphasethat hasformedandfortheliquidtodraintothebottomofthecellsothatonlygas-phasehydrocarbons areproducedfromthetopofthecell.Mercuryisinjectedintothebottomofthecellandgasis removedatthetopatsucharateastomaintainconstantpressureinthecell.Thusthevolumeof gasremoved,measuredatthislowerpressureandcell(reservoir)temperature,equalsthevolume ofmercuryinjectedwhenthehydrocarbonvolume,nowtwophase,isreturnedtotheinitialcell volume.Thevolumeofretrogradeliquidismeasured,andthecycle—expansiontoanextlower pressurefollowedbytheremovalofasecondincrementofgas—isrepeateddowntoanyselected abandonmentpressure.Eachincrementofgasremovedisanalyzedtofinditscomposition,andthe volumeofeachincrementofproducedgasismeasuredatsubatmosphericpressuretodetermine thestandardvolume,usingtheidealgaslaw.Fromthis,thegasdeviationfactoratcellpressureand temperaturemaybecalculatedusingtherealgaslaw.Alternatively,thegasdeviationfactoratcell pressureandtemperaturemaybecalculatedfromthecompositionoftheincrement. Figure5.4andTable5.3givethecompositionofaretrogradegas-condensatereservoirfluidatinitialpressureandthecompositionofthegasremovedfromapressure-volume-temperature (PVT)cellineachoffiveincrements,aspreviouslydescribed.Table5.3alsogivesthevolumeof retrogradeliquidinthecellateachpressureandthegasdeviationfactorandvolumeoftheproduced gasincrementsatcellpressureandtemperature.AsshowninFig.5.4,theproducedgascomposition changesasthepressureofthecelldecreases.Forexample,2500psiashowsasubstantialdecreasein themolefractionoftheheptanes-plus,asmallerdecreaseforthehexanes,evensmallerforpentanes, andsoon,comparedtothe3000psiacomposition.Thelighterhydrocarbonshaveacorresponding 5.3 The Performance of Volumetric Reservoirs 133 increaseintheirmolefractionofthecompositionoverthatsameinterval.Thetrendisfortheheavier hydrocarbonstoselectivelycondenseinthecell,and,therefore,theyarenotproduced.Asthecell continuestobedepleted,thepressurereachesthepoint,asshownbypointB2inFig.1.4,whenthe heaviercomponentsbegintorevaporize.Forthisreason,asshowninFig.5.4andTable5.3,thetrend fromthe1000psiatothe500psiaincrementsshowsanincreaseofthemolefractionoftheheavier hydrocarbonsandadecreaseinthemolefractionofthelighterhydrocarbons. Theliquidrecoveryfromthegasincrementsproducedfromthecellmaybemeasuredbypassingthegasthroughsmall-scaleseparators,oritmaybecalculatedfromthecompositionforusual fieldseparationmethodsorforgasolineplantmethods.8,9,10Liquidrecoveryofthepentanes-plusis somewhatgreateringasolineplantsthaninfieldseparationandmuchgreaterforthepropanesand butanes,commonlycalledliquefiedpetroleumgas(LPG).Forsimplicity,theliquidrecoveryfromthe 1.0 C1 0.8 0.6 Composition, mole fraction 0.4 0.2 0.10 C2 0.08 0.06 C3 0.04 C4 C+7 0.02 C5 C6 0.01 Figure 5.4 0 500 1000 1500 2000 Pressure, psia 2500 3000 Variations in the composition of the produced gas phase material of a retrograde gas-condensate fluid with pressure decline (data from Table 5.3). Chapter 5 134 • Gas-Condensate Reservoirs gasincrementsofTable5.3iscalculatedinExample5.3,assuming25%ofthebutanes,50%ofthe pentanes,75%ofthehexanes,and100%oftheheptanes-plusarerecoveredasliquid. Example 5.3 Calculating the Volumetric Depletion Performance of a Retrograde GasCondensate Reservoir Based on the Laboratory Tests Given in Table 5.3 Given Initialpressure(dewpoint)=2960psia Abandonmentpressure=500psia Reservoirtemperature=195°F Connatewater=30% Porosity=25% Standardconditions=14.7psiaand60°F Initialcellvolume=947.5cm3 MolecularweightofC7+ininitialfluid=114lb/lb-mol SpecificgravityofC7+ininitialfluid=0.755at60°F Compositions,volumes,anddeviationfactorsgiveninTable5.3 AssumethesamemolecularweightandspecificgravityfortheC7+contentforallproducedgas. Alsoassumeliquidrecoveryfromthegasis25%ofthebutanes,50%ofthepentanes,75%ofthe hexanes,and100%oftheheptanesandheaviergases. Solution NotethatcolumnnumbersrefertoTable5.4. 1. CalculatetheincrementsofgrossproductioninMSCFperac-ftofnet,bulkreservoirrock. First,calculateVHC,thehydrocarbonvolumeperacre-ftofreservoir.Enterthefollowingin column2: VHC=43,560×0.25×(1–0.30)=7623ft3/ac-ft Fortheincrementproducedfrom2960to2500psia,forexample,thehydrocarbon volumewillbemultipliedbytheratiooftheproducedgas(fromTable5.3)tothecell volumegiven.Thatvolumeisthenconvertedtostandardunitsasshown. ΔV = 7623 × Gp = 175.3cucm = 1410 ft 3 /ac-ft at2500psiaand195°F 947.5 cucm 379.4 pV 379.4 × 2500 × 1410 = = 239.7 MSCF/ac-ft 1000 zRT 1000 × 0.794 × 10.773 × 655 Findthecumulativegrossgasproduction,Gp = ΣΔGp,andenterincolumn3. Table 5.3 Volume, Composition, and Gas Deviation Factors for a Retrograde Condensate Fluid (1) Pressure (psia) (2) (3) (4) (5) (6) (7) (8) Composition of produced gas increments (mole fraction) (9) (10) (11) (12) Produced gas (cm3 at 195 °F and cell pressure) Retrograde liquid volume (cm3 cell volume, 947.5 cm3) Retrograde volume (percent of hydrocarbon volume) Gas deviation factor (at 195°F and cell pressure) 135 C1 C2 C3 C4 C5 C6 C7+ 2960 0.752 0.077 0.044 0.031 0.022 0.022 0.052 0.0 0.0 0.0 0.771 2500 0.783 0.077 0.043 0.028 0.019 0.016 0.034 175.3 62.5 6.6 0.794 2000 0.795 0.078 0.042 0.027 0.017 0.014 0.027 227.0 77.7 8.2 0.805 1500 0.798 0.079 0.042 0.027 0.016 0.013 0.025 340.4 75.0 7.9 0.835 1000 0.793 0.080 0.043 0.028 0.017 0.013 0.026 544.7 67.2 7.1 0.875 500 0.768 0.082 0.048 0.033 0.021 0.015 0.033 1080.7 56.9 6.0 0.945 Table 5.4 Gas and Liquid Recoveries in Percentage and per Acre-Foot for Example 5.3 136 (1) (2) (3) (4) (5) (6) (7) (8) (9) (10) (11) Pressure (psia) Increments of gross gas production (M SCF) Cumulative gross gas production (M SCF), Σ(2) Residue gas in each increment (M SCF) Cumulative residue gas production (M SCF), Σ(4) Liquid in each increment (bbl) Cumulative liquid production (bbl), Σ(6) Average gas-oil ratio of each increment (SCF residue gas per bbl), (4) ÷ (6) Cumulative gross gas recovery (percentage), (3) × 100/1580 Cumulative residue gas recovery (percentage), (5) × 100/1441 Cumulative liquid recovery (percentage), (7) × 100/ 143.2 2960 0 0 0 0 0 0 0 0 0 2500 239.7201 239.7201 224.7376 224.7376 15.3182 15.3182 14,671 15.1722 15.5959 10.6971 2000 248.3352 488.0553 235.2356 459.9731 13.2680 28.5863 17,729 30.8896 31.9204 19.9625 1500 279.2951 767.3504 265.4700 725.4431 13.9622 42.5485 19,013 48.5665 50.3430 29.7127 1000 297.9476 1065.2980 282.6778 1008.1209 15.4188 57.9673 18,333 67.4239 69.9598 40.4800 500 295.5682 1360.8662 276.9474 1285.0683 18.8721 76.8394 14,675 86.1308 89.1789 53.6588 5.3 The Performance of Volumetric Reservoirs 137 2. CalculatetheMSCFofresiduegasandthebarrelsofliquidobtainedfromeach incrementofgrossgasproduction.Enterincolumns4and6.Assumethat25%ofC4, 50%ofC5,75%ofC6, and all C7+arerecoveredasstock-tankliquid.Forexample,in the239.7MSCFproducedfrom2960to2500psia,themolefractionrecoveredas liquidis ΔnL=0.25×0.028+0.50×0.019+0.75×0.016+0.034 =0.0070+0.0095+0.0120+0.034=0.0625molefraction Asthemolefractionalsoequalsthevolumefractioningas,theMSCFrecovered asliquidfrom239.7MSCFis ΔGL=0.0070×239.7+0.0095×239.7+0.0120×239.7+0.034×239.7 =1.681+2.281+2.881+8.163=14.981MSCF Thegasvolumecanbeconvertedtogallonsofliquidusingthegal/MSCFfigures ofTable2.1forC4, C5, and C6.Theaverageoftheiso-andnormalcompoundsisusedfor C4 and C5. ForC7+, 114 lb/lb-mol = 47.71gal/MSCF 0.379 MSCF/lb-mol × 8.337 lb/gal × 0.755 0.3794isthemolarvolumeatstandardconditionsof14.7psiaand60°F.Thenthetotal liquidrecoveredfrom239.7MSCFis1.681×32.04+2.281×36.32+2.881×41.03+ 8.163×47.71=53.9+82.8+118.2+389.5=644.4gal=15.3STB.Theresiduegas recoveredfromthe239.7MSCFis239.7×(1–0.0625)=224.7MSCF.Calculatethe cumulativeresiduegasandstock-tankliquidrecoveriesfromcolumns4and6andenter incolumns5and7,respectively. 3. Calculatethegas-oilratioforeachincrementofgrossproductioninunitsofresiduegas perbarrelofliquid.Enterincolumn8.Forexample,thegas-oilratiooftheincrement producedfrom2960to2500psiais 224.7 × 1000 = 14, 686 SCF/STB 15.3 4. Calculatethecumulativerecoverypercentagesofgrossgas,residuegas,andliquid.Enter incolumns9,10,and11.Theinitialgrossgasinplaceis Chapter 5 138 • Gas-Condensate Reservoirs 379.4 pV 379.4 × 2960 × 7623 = = 1580 MSCF/ac-ft 1000 zRT 1000 × 0.771 × 10.73 × 6655 Ofthis,theliquidmolefractionis0.088andthetotalliquidrecoveryis3.808 gal/MSCFofgrossgas,whicharecalculatedfromtheinitialcompositioninthesame mannershowninpart2.Then G=(1–0.088)×1580=1441MSCFresiduegas/ac-ft N= 3.808 × 1580 = 143.2 STB/ac-ft 42 At2500psia,then Gross gas recovery percent= 10 × 23.7 = 1.2% 158 Residuegas recovery percent= Liquidrecovery percent= 10 × 22.7 = 1.6% 144 100 × 15.3 = 10.7% 143.2 TheresultsofthelaboratorytestsandcalculationsofExample5.3areplottedversuspressure inFig.5.5.Thegas-oilratiorisessharplyfrom10,060SCF/bbltoabout19,000SCF/bblnear1600 psia.Maximumretrogradeliquidandmaximumgas-oilratiosdonotoccuratthesamepressure because,aspointedoutpreviously,theretrogradeliquidvolumeismuchlargerthanitsequivalent obtainablestock-tankvolume,andthereismorestock-tankliquidin6.0%retrogradeliquidvolume at500psiathanin7.9%at1500psia.Revaporizationbelow1600psiahelpsreducethegas-oil ratio.However,thereissomedoubtthatrevaporizationequilibriumisreachedinthereservoir;the fieldgas-oilratiosgenerallyremainhigherthanthatpredicted.Partofthisisprobablyaresultof thelowerseparatorefficiencyofliquidrecoveryatthelowerpressureandhigherseparatortemperatures.Lowerseparatortemperaturesoccurathigherwellheadpressures,owingtothegreater coolingofthegasbyfreeexpansioninflowingthroughthechoke.Althoughtheoverallrecovery at500-psiaabandonmentpressureis86.1%,theliquidrecoveryisonly53.7%,owingtoretrograde condensation.Thecumulativeproductionplotsareslightlycurvedbecauseofthevariationinthe gasdeviationfactorwithpressureandwiththecompositionofthereservoirfluid. The volumetric depletion performance of a retrograde condensate fluid, such as given in Example 5.3, may also be calculated from the initial composition of the single-phase reservoir fluid,usingequilibriumratios.Anequilibriumratio(K)istheratioofthemolefraction(y)ofany 5.3 The Performance of Volumetric Reservoirs 139 componentinthevaporphasetothemolefraction(x)ofthesamecomponentintheliquidphase, or K = y/x.Theseratiosdependonthetemperatureandpressureand,unfortunately,onthecompositionofthesystem.Ifasetofequilibriumratioscanbefoundthatareapplicabletoagivencondensatesystem,thenitispossibletocalculatethemoledistributionbetweentheliquidandvapor phasesatanypressureandreservoirtemperatureandalsothecompositionoftheseparatevapor andliquidphases,asshowninFig.5.4.Fromthecompositionandtotalmolesineachphase,itis alsopossibletocalculatewithreasonableaccuracytheliquidandvaporvolumesatanypressure. Thepredictionofretrogradecondensateperformanceusingequilibriumratiosisaspecialized technique.StandingandRodgers,Harrison,andRegiergavemethodsforadjustingpublishedequilibriumratiodataforcondensatesystemstoapplytosystemsofdifferentcompositions.4,8,11,12,13,14 Theyalsogavestep-by-stepcalculationmethodsforvolumetricperformance,startingwithaunit volumeoftheinitialreservoirvaporofknowncomposition.Anincrementofvaporphasematerial isassumedtoberemovedfromtheinitialvolumeatconstantpressure,andtheremainingfluidis expandedtotheinitialvolume.Thefinalpressure,thedivisioninvolumebetweenthevaporand 20 2960 psia atio oil r Gas- 16 14,650 SCF/bbl 1271 MCF 1200 MCF 12 Cu mu lat Cu mu lat ive ive res to tal idu 8 Retrograde liquid eg 71.6 bbl as 6.0% Cum ulat 4 0 0 Figure 5.5 500 1000 ive oil 1500 Pressure, psia 2000 2500 3000 Gas-oil ratios, retrograde liquid volumes, and recoveries for the depletion performance of a retrograde gas-condensate reservoir (data from Tables 5.3 and 5.4). Chapter 5 140 • Gas-Condensate Reservoirs retrogradeliquidphases,andtheindividualcompositionsofthevaporandliquidphasesarethen calculatedusingtheadjustedequilibriumratios.Asecondincrementofvaporisremovedatthe lowerpressure,andthepressure,volumes,andcompositionsarecalculatedasbefore.Anaccountis keptoftheproducedmolesofeachcomponentsothatthetotalmolesofanycomponentremaining atanypressureareknownbysubtractionfromtheinitialamount.Thiscalculationmaybecontinueddowntoanyabandonmentpressure,justasinthelaboratorytechnique. Standingpointsoutthatthepredictionofcondensatereservoirperformancefromequilibrium ratiosaloneislikelytobeinconsiderableerrorandthatsomelaboratorydatashouldbeavailableto checktheaccuracyoftheadjustedequilibriumratios.4Actually,theequilibriumratiosarechanging becausethecompositionofthesystemremaininginthereservoirorcellchanges.Thechangesin thecompositionoftheheptanes-plusparticularlyaffectthecalculations.Rodgers,Harrison,and Regierpointouttheneedforimprovedproceduresfordevelopingtheequilibriumratiosforthe heavierhydrocarbonstoimprovetheoverallaccuracyofthecalculation.8 Jacoby, Koeller, and Berry studied the phase behavior of eight mixtures of separator oil andgasfromaleangas-condensatereservoiratrecombinedratiosintherangeof2000to25,000 SCF/STBandatseveraltemperaturesintherangeof100°Fto250°F.15Theresultsareusefulin predicting the depletion performance of gas-condensate reservoirs for which laboratory studies arenotavailable.Theyshowthatthereisagradualchangeinthesurfaceproductionperformance fromthevolatileoiltotherichgas-condensatetypeofreservoirandthatalaboratoryexamination isnecessarytodistinguishbetweenthedew-pointandbubble-pointreservoirsintherangeof2000 to6000SCF/STBgas-oilratios. 5.4 Use of Material Balance ThelaboratorytestontheretrogradecondensatefluidinExample5.3isitselfamaterialbalance studyofthevolumetricperformanceofthereservoirfromwhichthesamplewastaken.Theapplication of the basic data and the calculated data of Example 5.3 to a volumetric reservoir is straightforward.Forexample,supposethereservoirhadproduced12.05MMMSCFofgrosswell fluidwhentheaveragereservoirpressuredeclinedfrom2960psiainitialto2500psia.According toTable5.4,therecoveryat2500psiaundervolumetricdepletionis15.2%oftheinitialgrossgas inplace,andthereforetheinitialgrossgasinplaceis G= 12.05 × 10 9 = 79.28 MMMSCF 0.152 BecauseTable5.4showsarecoveryof80.4%downtoanabandonmentpressureof500psia,the initialrecoverablegrossgasortheinitialreserve is Initialreserve=79.28×109 ×0.804=63.74MMMSCF Since12.05MMMSCFhasalreadybeenrecovered,thereserveat2500psiais 5.4 Use of Material Balance 141 Reserveat2500psia=63.74–12.05=51.69MMMSCF Theaccuracyofthesecalculationsdepends,amongotherthings,onthesamplingaccuracyand thedegreeofwhichthelaboratorytestrepresentsthevolumetricperformance.Generallythereare pressuregradientsthroughoutareservoirtoindicatethatthevariousportionsofthereservoirare invaryingstagesofdepletion.Thisisduetogreaterwithdrawalsinsomeportionsand/ortolower reservesinsomeportionsbecauseoflowerporositiesand/orlowernetproductivethicknesses.Asa consequence,thegas-oilratiosofthewellsdiffer,andtheaveragecompositionofthetotalreservoir productionatanyprevailingaveragereservoirpressuredoesnotexactlyequalthecompositionof thetotalcellproductionatthesamepressure. Althoughthegrossgasproductionhistoryofavolumetricreservoirfollowsthelaboratory testsmoreorlessclosely,thedivisionoftheproductionintoresiduegasandliquidfollowswith lessaccuracy.Thisisduetothedifferencesinthestageofdepletionofvariousportionsofthereservoir,asexplainedintheprecedingparagraph,andalsotothedifferencesbetweenthecalculated liquidrecoveriesinthelaboratorytestsandtheactualefficiencyofseparatorsinrecoveringliquid fromthefluidinthefield. Thepreviousremarksapplyonlytovolumetricsingle-phasegas-condensatereservoirs.Unfortunately, most retrograde gas-condensate reservoirs that have been discovered are initially at their dew-point pressures rather than above them.This indicates the presence of an oil zone in contactwiththegas-condensatecap.Theoilzonemaybenegligiblysmallorcommensuratewith thesizeofthecap,oritmaybemuchlarger.Thepresenceofasmalloilzoneaffectstheaccuracy ofthecalculationsbasedonthesingle-phasestudyandismoreseriousforalargeroilzone.When theoilzoneisofasizeatallcommensuratewiththegascap,thetwomustbetreatedtogetherasa two-phasereservoir,asexplainedinChapter7. Many gas-condensate reservoirs are produced under a partial or total water drive.When the reservoirpressurestabilizesorstopsdeclining,asoccursinmanyreservoirs,recoverydependsonthe valueofthepressureatstabilizationandtheefficiencywithwhichtheinvadingwaterdisplacesthegas phasefromtherock.Theliquidrecoveryislowerforthegreaterretrogradecondensationbecausethe retrogradeliquidisgenerallyimmobileandistrappedtogetherwithsomegasbehindtheinvadingwaterfront.Thissituationisaggravatedbypermeabilityvariationsbecausethewellsbecome“drowned” andareforcedoffproductionbeforethelesspermeablestrataaredepleted.Inmanycases,therecovery bywaterdriveislessthanbyvolumetricperformance,asexplainedinChapter4,section3.4. Whenanoilzoneisabsentornegligible,thematerialbalanceEq.(4.13)maybeapplied toretrogradereservoirsunderbothvolumetricandwater-driveperformance,justasforthesingle-phase(nonretrograde)gasreservoirsforwhichitwasdeveloped: G(Bg – Bgi) + We = GpBg + BwWp (4.13) Thisequationmaybeusedtofindeitherthewaterinflux,We,ortheinitialgasinplace,G.The equationcontainsthegasdeviationfactorzatthelowerpressure.Itisincludedinthegasvolume factorBginEq.(4.13).Becausethisdeviationfactorappliestothegas-condensatefluidremaining Chapter 5 142 • Gas-Condensate Reservoirs inthereservoir,whenthepressureisbelowthedew-pointpressureinretrogradereservoirs,itis a two-phasegasdeviationfactor.TheactualvolumeinEq.(2.7)includesthevolumeofboththe gasandliquidphases,andtheidealvolumeiscalculatedfromthetotalmolesofgasandliquid, assuming ideal gas behavior. For volumetric performance, this two-phase deviation factor may beobtainedfromsuchlaboratorydataasobtainedinExample5.3.Forexample,fromthedataof Table5.5,thecumulativegrossgasproductiondownto2000psiais485.3MSCF/ac-ftoutofan initialcontentof1580MSCF/ac-ft.Sincetheinitialhydrocarbonporevolumeis7623ft3/ac-ft (Example5.3),thetwo-phasevolumefactorforthefluidremaininginthereservoirat2000psia and195°Fascalculatedusingthegaslawis z= 379.4 × pV 379.4 × 2000 × 7623 = 0.752 = (G − G p ) R ' T (1580 − 485.3)110 3 × 10.73 × 655 Table5.5givesthetwo-phasegasdeviationfactorsforthefluidremaininginthereservoiratpressuresdownto500psia,calculatedasbeforeforthegas-condensatefluidofExample5.3.These dataarenotstrictlyapplicablewhenthereissomewaterinfluxbecausetheyarebasedoncellperformanceinwhichvaporequilibriumismaintainedbetweenallthegasandliquidremaininginthe cell,whereasinthereservoir,someofthegasandretrogradeliquidsareenvelopedbytheinvading waterandarepreventedfromenteringintoequilibriumwiththehydrocarbonsintherestofthe reservoir.ThedeviationfactorsinTable5.5,column4,maybeusedwithvolumetricreservoirsand, withsomereductioninaccuracy,withwater-drivereservoirs. WhenlaboratorydatasuchasthosegiveninExample5.3havenotbeenobtained,thegas deviationfactorsoftheinitialreservoirgasmaybeusedtoapproximatethoseoftheremaining Table 5.5 (1) Two-Phase and Single-Phase Gas Deviation Factors for the Retrograde GasCondensate Fluid of Example 5.3 (2) (3) (4) (5) (6) Gas deviation factors Gpa (M SCF/ac-ft) (G – Gp )a (M SCF/ac-ft) Two-phaseb Initial gasc Produced gasa 2960 0.0 1580.0 0.771 0.780 0.771 2500 240.1 1339.9 0.768 0.755 0.794 2000 485.3 1094.7 0.752 0.755 0.805 1500 751.3 828.7 0.745 0.790 0.835 1000 1022.1 557.9 0.738 0.845 0.875 500 1270.8 309.2 0.666 0.920 0.945 Pressure (psia) DatafromTable5.4andExample5.3. CalculatedfromthedataofTable5.4andExample5.3. c Calculatedfrominitialgascompositionusingcorrelationcharts. a b 5.5 Comparison between the Predicted and Actual Production Histories 143 reservoirfluid.Thesearebestmeasuredinthelaboratorybutmaybeestimatedfromtheinitialgas gravityorwell-streamcompositionusingthepseudoreducedcorrelations.Althoughthemeasured deviationfactorsfortheinitialgasofExample5.3arenotavailable,itisbelievedthattheyare closertothetwo-phasefactorsincolumn4thanthosegivenincolumn5ofTable5.5,whichare calculated using the pseudoreduced correlations, since the latter method presumes single-phase gases.Thedeviationfactorsoftheproducedgasphasearegivenincolumn6forcomparison. 5.5 Comparison between the Predicted and Actual Production Histories of Volumetric Reservoirs Average gas rate, thousand MCF per month 4000 Pressure 10 2000 Number of wells 700 0 600 500 400 300 Gas rate 200 100 0 Figure 5.6 20 3000 Number of wells Reservoir pressure, psia at –7200 ft AllenandRoehavereportedtheperformanceofaretrogradecondensatereservoirthatproducesfrom theBaconLimeZoneofafieldlocatedinEastTexas.13Theproductionhistoryofthisreservoiris showninFigs.5.6and5.7.ThereservoiroccursinthelowerGlenRoseFormationofCretaceousage atadepthof7600ft(7200ftsubsea)andcomprisessome3100acres.Itiscomposedofapproximately 50ftofdense,crystalline,fossiliferousdolomite,withanaveragepermeabilityof30to40millidarcys inthemorepermeablestringersandanestimatedaverageporosityofabout10%.Interstitialwater isapproximately30%.Thereservoirtemperatureis220°F,andtheinitialpressurewas3691psiaat 7200ftsubsea.Becausethereservoirwasveryheterogeneousregardingporosityandpermeability, and because very poor communication between wells was observed, cycling (section 5.6) was not 1941 1942 1943 1944 1945 Years 1946 1947 1948 1949 Production history of the Bacon Lime Zone of an eastern Texas gas-condensate reservoir (after Allen and Roe, trans. AlME).13 Chapter 5 144 • Gas-Condensate Reservoirs 4500 3500 p/z 3000 Solid lines—calculated theoretical pressures 2500 p Data point—field pressure surveys 2000 6 1500 4 1000 GPM 2 500 0 Figure 5.7 0 2 4 6 8 10 12 14 16 18 20 22 Cumulative wet gas recovery, million standard MCF 0 24 Recovery rate stock tank liquid, GPM (average of 3 month periods) Reservoir pressure, psia at –7200 ft 4000 Calculated and measured pressure and p/z values versus cumulative gross gas recovery from the Bacon Lime Zone of an eastern Texas gas-condensate reservoir (after Allen and Roe, trans. AlME).13 considered feasible.The reservoir was therefore produced by pressure depletion, using three-stage separationtorecoverthecondensate.Therecoveryat600psiawas20,500MMSCFand830,000bbl ofcondensate,oracumulative(average)gas-oilratioof24,700SCF/bbl,or1.70GPM(gallonsper MCF).Sincetheinitialgas-oilratioswereabout12,000SCF/bbl(3.50GPM),thecondensaterecovery of600psiawas100×1.7/3.5,or48.6%oftheliquidoriginallycontainedintheproducedgas.Theoreticalcalculationsbasedonequilibriumratiospredictedarecoveryofonly1.54GPM(27,300gas-oil ratio),or44%recovery,whichisabout10%lower. Thedifferencebetweentheactualandpredictedrecoveriesmayhavebeenduetosampling errors.Theinitialwellsamplesmayhavebeendeficientintheheavierhydrocarbons,owingtoretrogradecondensationofliquidfromtheflowingfluidasitapproachedthewellbore(section5.3). AnotherpossibilitysuggestedbyAllenandRoeistheomissionofnitrogenasaconstituentofthe gasfromthecalculations.Asmallamountofnitrogen,alwaysbelow1mol%,wasfoundinseveral ofthesamplesduringthelifeofthereservoir.Finally,theysuggestedthepossibilityofretrograde liquidflowinthereservoirtoaccountforaliquidrecoveryhigherthanthatpredictedbytheirtheoreticalcalculations,whichpresumetheimmobilityoftheretrogradeliquidphase.Consideringthe manyvariablesthatinfluenceboththecalculatedrecoveryusingequilibriumratiosandthefield performance,theagreementbetweenthetwoappearsgood. Figure5.8showsgoodgeneralagreementbetweenthebutanes-pluscontentcalculatedfrom thecompositionoftheproductionfromtwowellsandthecontentcalculatedfromthestudybasedon 5.5 Comparison between the Predicted and Actual Production Histories 145 Well-stream effluent, GPM butanes-plus 5 4 Companion sample analyses (Well 2) (Well 1) 3 2 Calculated differential Calculated flash 1 0 0 Figure 5.8 400 800 1200 1600 2000 2400 2800 Reservoir pressure, psia at –7200 ft 3200 3600 4000 Calculated and measured butanes-plus in the well streams of the Bacon Lime Zone of an eastern Texas gas-condensate reservoir (after Allen and Roe, trans. AlME).13 equilibriumratios.Theliquidcontentexpressedinbutanes-plusishigherthanthestock-tankGPM (Fig.5.7)becausenotallthebutanes—or,forthatmatter,allthepentanes-plus—arerecoveredinthe fieldseparators.Thehigheractualbutanes-pluscontentdownto1600psiaisundoubtedlyaresult ofthesamecausesgivenintheprecedingparagraphtoexplainwhytheactualoverallrecoveryof stock-tankliquidexceededtherecoverybasedonequilibriumratios.Thestock-tankGPMinFig.5.7 showsnorevaporization;however,thewell-streamcompositionsbelow1600psiainFig.5.8clearly showrevaporizationofthebutanes-plus,andthereforecertainlyofthepentanes-plus,whichmakeup themajorityoftheseparatorliquid.Therevaporizationoftheretrogradeliquidinthereservoirbelow 1600psiaisevidentlyjustaboutoffsetbythedecreaseinseparatorefficiencyatlowerpressures. Figure 5.8 also shows a comparison between the calculated reservoir behavior based on thedifferential processandtheflash process.Inthedifferential process,onlythegasisproduced andisthereforeremovedfromcontactwiththeliquidphaseinthereservoir.Intheflash process, allthegasremainsincontactwiththeretrogradeliquid,andforthis,thevolumeofthesystem mustincreaseasthepressuredeclines.Thusthedifferentialprocessisoneofconstantvolumeand changingcomposition,andtheflashprocessisoneofconstantcompositionandchangingvolume. Laboratoryworkandcalculationsbasedonequilibriumratiosaresimplerwiththeflashprocess, wheretheoverallcompositionofthesystemremainsconstant;however,thereservoirmechanism forthevolumetricdepletionofretrogradecondensatereservoirsisessentiallyadifferentialprocess. Thelaboratoryworkandtheuseofequilibriumratiosdiscussedinsection5.3anddemonstrated in Example 5.3 approaches the differential process by a series of step-by-step flash processes. Figure5.8showsthecloseagreementbetweentheflashanddifferentialcalculationsdownto1600 psia.Below1600psia,thewellperformanceisclosertothedifferentialcalculationsbecausethe Chapter 5 146 • Gas-Condensate Reservoirs 350 300 Reservoir data Laboratory data Gas-oil ratio, MCF per STB 250 200 150 100 50 0 0 Figure 5.9 500 1000 1500 2000 Pressure, psia 2500 3000 Comparison of field and laboratory data for a Paradox limestone gas-condensate reservoir in Utah (after Rodgers, Harrison, and Regier, courtesy AlME). 8 reservoirmechanismlargelyfollowsthedifferentialprocess,providedthatonlygasphasematerialsareproducedfromthereservoir(i.e.,theretrogradeliquidisimmobile). Figure5.9showsthegoodagreementbetweenthereservoirfielddataandthelaboratorydata forasmall(onewell),noncommercial,gas-condensateaccumulationintheParadoxlimestoneformationatadepthof5775ftinSanJuanCounty,Utah.ThisaffordedRodgers,Harrison,andRegier auniqueopportunitytocomparelaboratoryPVTstudiesandstudiesbasedonequilibriumratioswith actualfielddepletionundercloselycontrolledandobservedconditions.8Inthelaboratory,a4000cm3 cellwaschargedwithrepresentativewellsamplesatreservoirtemperatureandinitialreservoirpressure.Thecellwaspressuredepletedsothatonlythegasphasewasremoved,andtheproducedgas waspassedthroughminiaturethree-stageseparators,whichwereoperatedatoptimumfieldpressures 5.6 Lean Gas Cycling and Water Drive 147 andtemperatures.Thecalculatedperformancewasalsoobtained,asexplainedpreviously,fromequationsinvolvingequilibriumratios,assumingthedifferentialprocess.Rodgersetal.concludedthatthe modellaboratorystudycouldadequatelyreproduceandpredictthebehaviorofcondensatereservoirs. Also,theyfoundthattheperformancecouldbecalculatedfromthecompositionoftheinitialreservoirfluid,providedrepresentativeequilibriumratiosareavailable. Table5.6showsacomparisonbetweentheinitialcompositionsoftheBaconLimeandParadoxlimestoneformationfluids.Thelowergas-oilratiosfortheBaconLimeareconsistentwiththe BaconLimefluid’smuchlargerconcentrationofthepentanesandheaviergases. 5.6 Lean Gas Cycling and Water Drive Becausetheliquidcontentofmanycondensatereservoirsisavaluableandimportantpartofthe accumulationandbecausethroughretrogradecondensationalargefractionofthisliquidmaybe leftinthereservoiratabandonment,thepracticeofleangascyclinghasbeenadoptedinmanycondensatereservoirs.Ingascycling,thecondensateliquidisremovedfromtheproduced(wet)gas, usuallyinagasolineplant,andtheresidue,ordrygas,isreturnedtothereservoirthroughinjection wells.Theinjectedgasmaintainsreservoirpressureandretardsretrogradecondensation.Atthe sametime,itdrivesthewetgastowardtheproducingwells.Becausetheremovedliquidsrepresent partofthewetgasvolume,unlessadditionaldry(makeup)gasisinjected,reservoirpressurewill declineslowly.Attheconclusionofcycling(i.e.,whentheproducingwellshavebeeninvadedby thedrygas),thereservoiristhenpressuredepleted(blowndown)torecoverthegasplussomeof theremainingliquidsfromtheportionsnotswept. Althoughleangascyclingappearstobeanidealsolutiontotheretrogradecondensateproblem,anumberofpracticalconsiderationsmakeitlessattractive.First,thereisthedeferredincome fromthesaleofthegas,whichmaynotbeproducedfor10to20years.Second,cyclingrequires additionalexpenditures,usuallysomemorewells,agascompressionanddistributionsystemto theinjectionwells,andaliquidrecoveryplant.Third,itmustberealizedthatevenwhenreservoir pressureismaintainedabovethedewpoint,theliquidrecoverybycyclingmaybeconsiderably lessthan100%. Cyclingrecoveriescanbebrokendownintothreeseparaterecoveryfactors,orefficiencies. Whendrygasdisplaceswetgaswithintheporesofthereservoirrock,themicroscopicdisplacement efficiencyisintherangeof70%to90%.Then,owingtothelocationandflowratesoftheproductionandinjectionwells,thereareareasofthereservoirthatarenotsweptbydrygasatthetimethe producingwellshavebeeninvadedbydrygas,resultinginsweepefficienciesintherangeof50%to 90%(i.e.,50%to90%oftheinitialporevolumeisinvadedbydrygas).Finally,manyreservoirsare stratifiedinsuchawaythatsomestringersaremuchmorepermeablethanothers,sothatthedrygas sweepsthroughthemquiterapidly.Althoughconsiderablewetgasremainsinthelowerpermeability (tighter)stringers,drygaswillhaveenteredtheproducingwellsinthemorepermeablestringers, eventuallyreducingtheliquidcontentofthegastotheplanttoanunprofitablelevel. Nowsupposeaparticulargas-condensatereservoirhasadisplacementefficiencyof80%, asweepefficiencyof80%,andapermeabilitystratificationfactorof80%.Theproductofthese Chapter 5 148 • Gas-Condensate Reservoirs Table 5.6 Comparison of the Compositions of the Initial Fluids in the Bacon Lime and Paradox Formations Bacon Lime Paradox formation ? 0.0099 Carbondioxide 0.0135 0.0000 Methane 0.7690 0.7741 Ethane 0.0770 0.1148 Propane 0.0335 0.0531 Butane 0.0350 0.0230 Pentane 0.0210 0.0097 Hexane 0.0150 0.0054 Heptanes-plus 0.0360 0.0100 Total 1.0000 1.0000 MolecularweightC 130 116.4 SpecificgravityC7 (60°F) 0.7615 0.7443 Nitrogen + 7 + separatefactorsisgivenanoverallcondensaterecoverybycyclingof51.2%.Undertheseconditions,cyclingmaynotbeparticularlyattractivebecauseretrogradecondensatelossesbydepletion performanceseldomexceed50%.However,duringpressuredepletion(blowdown)ofthereservoir following cycling, some additional liquid may be recovered from both the swept and unswept portionsofthereservoir.Also,liquidrecoveriesofpropaneandbutaneingasolineplantsaremuch higher than those from stage separation of low-temperature separation, which would be used if cyclingwasnotadopted.Fromwhathasbeensaid,itisevidentthatthequestionofwhetherto cycleinvolvesmanyfactorsthatmustbecarefullystudiedbeforeaproperdecisioncanbereached. Cyclingisalsoadoptedinnonretrogradegascapsoverlyingoilzones,particularlywhenthe oilisitselfunderlainbyanactivebodyofwater.Ifthegascapisproducedconcurrentlywiththe oil,asthewaterdrivestheoilzoneintotheshrinkinggascapzone,unrecoverableoilremainsnot onlyintheoriginaloilzonebutalsointhatportionofthegascapinvadedbytheoil.Ontheother hand,ifthegascapiscycledatessentiallyinitialpressure,theactivewaterdrivedisplacestheoil intotheproducingoilwellswithmaximumrecovery.Inthemeantime,someofthevaluableliquids fromthegascapmayberecoveredbycycling.Additionalbenefitswillaccrue,ofcourse,ifthegas capisretrograde.Evenwhenwaterdriveisabsent,theconcurrentdepletionofthegascapandthe oilzoneresultsinloweredoilrecoveries,andincreasedoilrecoveryisproducedbydepletingthe oilzonefirstandallowingthegascaptoexpandandsweepthroughtheoilzone. Whengas-condensatereservoirsareproducedunderanactivewaterdrivesuchthatreservoirpressuredeclinesverylittlebelowtheinitialpressure,thereislittleornoretrogradecondensation,andthegas-oilratiooftheproductionremainssubstantiallyconstant.Therecoveryisthe sameasinnonretrogradegasreservoirsunderthesameconditionsanddependson(1)theinitial 5.6 Lean Gas Cycling and Water Drive 149 connatewater,Swi;(2)theresidualgassaturation,Sgr,intheportionofthereservoirinvadedby water;and(3)thefraction,F,oftheinitialreservoirvolumeinvadedbywater.Thegasvolume factorBgiinft3/SCFremainssubstantiallyconstantbecausereservoirpressuredoesnotdecline, sothefractionalrecoveryis Recovery = Vi φ (1 − Swi − Sgr ) Bgi F Vi φ (1 − Swi ) Bgi = (1 − Swi − Sgr )F (5.4) (1 − Swi ) where Vi is the initial gross reservoir volume, Sgr is the residual gas saturation in the flooded area, Swiistheinitialconnatewatersaturation,andFisthefractionofthetotalvolumeinvaded. Table4.3showsthatresidualgassaturationslieinrangeof20%to50%followingwaterdisplacement.Thefractionofthetotalvolumeinvadedatanytimeoratabandonmentdependsprimarilyon welllocationandtheeffectofpermeabilitystratificationinedgewaterdrivesandwellspacingand thedegreeofwaterconinginbottomwaterdrives. Table5.7showstherecoveryfactorscalculatedfromEq.(5.4),assumingareasonablerange ofvaluesfortheconnatewater,residualgassaturation,andthefractionalinvasionbywateratabandonment.Therecoveryfactorsapplyequallytogasandgas-condensatereservoirsbecause,under activewaterdrive,thereisnoretrogradeloss. Table 5.7 Recovery Factors for Complete Water-Drive Reservoirs Based on Eq. (5.4) Sgr Sw F = 40 F = 60 F = 80 F = 90 F = 100 20 10 31.1 46.7 62.2 70.0 77.8 20 30.0 45.0 60.0 67.5 75.0 30 40 50 30 28.6 42.8 57.1 64.3 71.4 40 26.7 40.0 53.4 60.0 66.7 10 26.7 40.0 53.4 60.0 66.7 20 25.0 37.5 50.0 56.3 62.5 30 22.8 34.3 45.7 51.4 57.1 40 20.0 30.0 40.0 45.0 50.0 10 22.2 33.3 44.4 50.0 55.6 20 20.0 30.0 40.0 45.0 50.0 30 17.1 25.7 34.2 38.5 42.8 40 13.3 20.0 26.6 30.0 33.3 10 17.7 26.6 35.5 40.0 44.4 20 15.0 22.5 30.0 33.8 37.5 30 11.4 17.1 22.8 25.7 28.5 40 6.7 10.0 13.6 15.0 16.7 Chapter 5 150 Table 5.8 • Gas-Condensate Reservoirs Comparison of Gas-Condensate Recovery by Volumetric Performance, Complete Water Drive, and Partial Water Drive (Based on the Data of Tables 5.3 and 5.4 and Example 5.3. Sw = 30%; Sgr = Sor + Sgr = 20%; F = 80%) Gas recovery Gross recovery Recovery mechanism Condensate bbl/ ac-ft Recovery percentage MCF/ac-ft Percentage MCF/ac-ft Percentage Initialinplace 143.2 100.0 1441 100.0 1580 100.0 Depletionto 500psia 71.6 50.0 1200 83.3 1271 80.4 Waterdriveat 2960psia 81.8 57.1 823 57.1 902 57.1 (a)Depletionto 2000psia 28.4 19.8 457 31.7 485 30.7 (b)Waterdrive at2000psia 31.2 21.8 553 38.4 584 37.0 Totalbypartial waterdrive, (a)+(b) 59.6 41.6 1010 70.1 1069 67.7 Table5.8showsacomparisonofgas-condensaterecoveryforthereservoirofExample5.3 by(1)volumetricdepletion,(2)waterdriveatinitialpressureof2960psia,and(3)partialwater drivewherethepressurestabilizesat2000psia.Theinitialgrossfluid,gas,andcondensate,andthe recoveriesbydepletionperformanceatanassumedabandonmentpressureof500psia,areobtained fromExample5.3andTables5.3and5.4.Undercompletewaterdrive,therecoveryis57.1%fora residualgassaturationof20%,aconnatewaterof30%,andafractionalinvasionof80%atabandonment,asmaybefoundbyEq.(5.4)orTable5.7.Becausethereisnoretrogradeloss,thisfigure appliesequallytothegrossgas,gas,andcondensaterecovery. Whenapartialwaterdriveexistsandthereservoirpressurestabilizesatsomepressure, here 2000 psia, the recovery is approximately the sum of the recovery by pressure depletion downtothestabilizationpressure,plustherecoveryoftheremainingfluidbycompletewater driveatthestabilizationpressure.Becausetheretrogradeliquidatthestabilizationpressureis immobile,itisenvelopedbytheinvadingwater,andtheresidualhydrocarbonsaturation(gas plusretrogradeliquid)isaboutthesameasforgasalone,or20%forthisexample.Therecovery figuresofTable5.8bydepletiondownto2000psiaareobtainedfromTable5.4.Theadditional recoverybywaterdriveat2000psiamaybeexplainedusingthefiguresofTable5.9.At2000 psia,theretrogradecondensatevolumeis625ft3/ac-ft,or8.2%oftheinitialhydrocarbonpore volumeof7623ft3/ac-ft,8.2%beingfoundfromthePVTdatagiveninTable5.3.Iftheresidual hydrocarbon(bothgasandcondensate)saturationafterwaterinvasionisassumedtobe20%,as previouslyassumedfortheresidualgassaturationbycompletewaterdrive,thewatervolumeafterwaterdriveis80%of10,890,or8712ft3/ac-ft.Theremaining20%(2178ft3/ac-ft),assuming 5.6 Lean Gas Cycling and Water Drive 151 Table 5.9 Volumes of Water, Gas, and Condensate in 1 Acre-Foot of Bulk Rock for the Reservoir in Example 5.3 Initial reservoir volumes (ft3/ac-ft) Volumes after depletion to 2000 psia (ft3/ac-ft) Volumes after water drive at 2000 psia (ft3/ac-ft) Water 3267 3267 8712 Gas 7623 6998 1553 Condensate Total ... 625 625 10,890 10,890 10,890 pressurestabilizesat2000psia,willconsistof625ft3/ac-ftofcondensateliquidand1553ft3/ ac-ftoffreegas.Thereservoirvaporat2000psiapriortowaterdriveis 2000 × 6998 × 379.4 = 938.5 MSCF//ac-ft 1000 × 0.805 × 10.73 × 655 Thefractionalrecoveryofthisvaporphasebycompletewaterdriveat2000psiais 6998 − 1553 = 0.778 or77.8% 6998 IfF=0.80—oronly80%ofeachacre-foot,ontheaverage,isinvadedbywateratabandonment— theoverallrecoveryreducesto0.80×0.778,or62.2%ofthevaporcontentat2000psia,or584M SCF/ac-ft.Table5.4indicatesthat,at2000psia,theratioofgrossgastoresiduegasafterseparation is245.2to232.3andthatthegas-oilratioonaresiduegasbasisis17,730SCF/bbl.Thus584M SCFofgrossgascontainsresiduegasintheamountof 584 × 232.3 = 553 MSCF/ac-ft 245.2 andtankorsurfacecondensateliquidintheamountof 553 × 1000 = 31.2 bbl/ac-ft 17, 730 Table5.8indicatesthatforthegas-condensatereservoirofExample5.3,usingtheassumed valuesforF and Sgr,bestoverallrecoveryisobtainedbystraightdepletionperformance.Bestcondensaterecoveryisbyactivewaterdrivebecausenoretrogradeliquidforms.Thevalueoftheproducts obtaineddepends,ofcourse,ontherelativeunitpricesatwhichthegasandcondensatearesold. 152 5.7 Chapter 5 • Gas-Condensate Reservoirs Use of Nitrogen for Pressure Maintenance Oneofthemajordisadvantagesassociatedwiththeuseofleangasingas-cyclingapplicationsis thattheincomethatwouldbederivedfromthesaleoftheleangasisdeferredforseveralyears.For thisreason,theuseofnitrogenhasbeensuggestedasareplacementfortheleangas.16However, onemightexpectthephasebehaviorofnitrogenandawetgastoexhibitdifferentcharacteristics fromthatofleangasandthesamewetgas.Researchershavefoundthatmixingnitrogenanda typicalwetgascausesthedewpointoftheresultingmixturetobehigherthanthedewpointofthe originalwetgas.17,18Thisisalsotrueforleangas,butthedewpointisraisedhigherwithnitrogen.17 If,inareservoirsituation,thereservoirpressureisnotmaintainedhigherthanthisnewdewpoint, thenretrogradecondensationwilloccur.Thiscondensationmaybeasmuchormorethanwhat wouldoccurifthereservoirwasnotcycledwithgas.Studieshaveshown,however,thatverylittle mixingoccursbetweenaninjectedgasandthereservoirgasinthereservoir.17,18Mixingoccursas aresultofmoleculardiffusionanddispersionforces,andtheresultingmixingzonewidthisusuallyonlyafewfeet.19,20Thedewpointmayberaisedinthislocalareaofmixing,butthiswillbe averysmallvolumeand,asaresult,onlyasmallamountofcondensatemaydropout.Vogeland Yarboroughhavealsoshownthat,undercertainconditions,nitrogenrevaporizesthecondensate.18 Theconclusionfromthesestudiesindicatesthatnitrogencanbeusedasareplacementforleangas incyclingoperationswiththepotentialforsomecondensateformationthatshouldbeminimalin mostapplications. Kleinsteiber,Wendschlag,andCalvinconductedastudytodeterminetheoptimumplanof depletionfortheAnschutzRanchEastUnit,whichislocatedinSummitCounty,Utah,andUinta County,Wyoming.21 TheAnschutz Ranch East Field, discovered in 1979, is one of the largest hydrocarbon accumulations found in theWestern Overthrust Belt.Tests have indicated that the originalin-placehydrocarboncontentwasover800millionbblofoilequivalent.Laboratoryexperimentsconductedonseveralsurface-recombinedsamplesindicatedthatthereservoirfluidwas arichgascondensate.Thefluidhadadewpointonly150to300psiabelowtheoriginalreservoir pressureof5310psia.Thedew-pointpressurewasafunctionofthestructuralpositioninthereservoir,withfluidnearthewater-oilcontacthavingadewpointabout300psialowerthantheoriginal pressureandfieldnearthecresthavingadewpointonlyabout150psialower.Theliquidsaturation,observedinconstantcompositionexpansiontests,accumulatedveryrapidlybelowthedew point,suggestingthatdepletionofthereservoirandthesubsequentdropinreservoirpressurecould causethelossofsignificantamountsofcondensate.Becauseofthispotentiallossofvaluablehydrocarbons,aprojectwasundertakentodeterminetheoptimummethodofproduction.21 To begin the study, a modified Redlich-Kwong equation of state was calibrated with the laboratoryphasebehaviordatathathadbeenobtained.17,22Theequationofstatewasthenusedina compositionalreservoirsimulator.Severaldepletionschemeswereconsidered,includingprimary depletion and partial or full pressure maintenance.Wet hydrocarbon gas, dry hydrocarbon gas, carbondioxide,combustionfluegas,andnitrogenwereallconsideredaspotentialgasestoinject. Carbondioxideandfluegaswereeliminatedduetolackofavailabilityandhighcost.Theresults ofthestudyledtotheconclusionthatfullpressuremaintenanceshouldbeused.Liquidrecoveries were found to be better with dry hydrocarbon gas than with nitrogen. However, when nitrogen Problems 153 injectionwasprecededbya10%to20%bufferofdryhydrocarbongas,theliquidrecoverieswere nearlythesame.Whenaneconomicanalysiswascoupledwiththesimulationstudy,thedecision wastoconductafull-pressuremaintenanceprogramwithnitrogenastheinjectedgas.A10%pore volumebuffer,consistingof35%nitrogenand65%wethydrocarbongas,wastobeinjectedbefore thenitrogentoimprovetherecoveryofliquidcondensate. TheapproachtakeninthestudybyKleinsteiber,Wendschlag,andCalvinwouldbeappropriatefortheevaluationofanygas-condensatereservoir.Theconclusionsregardingwhichinjected material is best or whether a buffer would be necessary may be different for a reservoir gas of differentcomposition. Problems 5.1 Agas-condensatereservoirinitiallycontains1300MSCFofresidue(dryorsalesgas)peracrefootand115STBofcondensate.Gasrecoveryiscalculatedtobe85%andcondensaterecovery 58%bydepletionperformance.Calculatethevalueoftheinitialgasandcondensatereservesper acre-footifthecondensatesellsfor$95.00/bblandthegassellsfor$6.00per1000stdft3. 5.2 Awellproduces45.3STBofcondensateand742MSCFofsalesgasdaily.Thecondensate hasamolecularweightof121.2andagravityof52.0°APIat60°F. (a) Whatisthegas-oilratioonadrygasbasis? (b) Whatistheliquidcontentexpressedinbarrelspermillionstandardcubicfeetonadry gasbasis? (c) WhatistheliquidcontentexpressedinGPMonadrygasbasis? (d) Repeatparts(a),(b),and(c),expressingthefiguresonawet,orgross,gasbasis. 5.3 Theinitialdailyproductionfromagas-condensatereservoiris186STBofcondensate,3750 MSCFofhigh-pressuregas,and95MSCFofstock-tankgas.Thetankoilhasagravityof 51.2°APIat60°F.Thespecificgravityoftheseparatorgasis0.712,andthespecificgravity ofthestock-tankgasis1.30.Theinitialreservoirpressureis3480psia,andreservoirtemperatureis220°F.Averagehydrocarbonporosityis17.2%.Assumestandardconditionsof 14.7psiaand60°F. Whatistheaveragegravityoftheproducedgases? Whatistheinitialgas-oilratio? Estimatethemolecularweightofthecondensate. Calculatethespecificgravity(air=1.00)ofthetotalwellproduction. Calculatethegasdeviationfactoroftheinitialreservoirfluid(vapor)atinitialreservoir pressure. (f) Calculatetheinitialmolesinplaceperacre-foot. (g) Calculatethemolefractionthatisgasintheinitialreservoirfluid. (h) Calculatetheinitial(sales)gasandcondensateinplaceperacre-foot. (a) (b) (c) (d) (e) Chapter 5 154 • Gas-Condensate Reservoirs 5.4 (a) C alculate the gas deviation factor for the gas-condensate fluid, the composition of whichisgiveninTable1.3at5820psiaand265°F.UsethecriticalvaluesofC8forthe C7+fraction. (b) Ifhalfthebutanesandallthepentanesandheaviergasesarerecoveredasliquids,calculatethegas-oilratiooftheinitialproduction.Comparewiththemeasuredgas-oilratio. 5.5 Calculate the composition of the reservoir retrograde liquid at 2500 psia for the data of Tables 5.3 and 5.4 and Example 5.3.Assume the molecular weight of the heptanes-plus fractiontobethesameasfortheinitialreservoirfluid. 5.6 Estimate the gas and condensate recovery for the reservoir of Example 5.3 under partial water drive if reservoir pressure stabilizes at 2500 psia.Assume a residual hydrocarbon saturationof20%andF=52.5%. 5.7 Calculatetherecoveryfactorbycyclinginacondensatereservoirifthedisplacementefficiencyis85%,thesweepefficiencyis65%,andthepermeabilitystratificationfactoris60%. 5.8 Thefollowingdataaretakenfromastudyonarecombinedsampleofseparatorgasand separatorcondensateinaPVTcellwithaninitialhydrocarbonvolumeof3958.14cm3.The wetgasgal/MSCF(GPM)andtheresiduegas-oilratioswerecalculatedusingequilibrium ratiosforproductionthroughaseparatoroperatingat300psiaand70°F.Theinitialreservoirpressurewas4000psia,whichwasalsoclosetothedew-pointpressure,andreservoir temperaturewas186°F. (a) Onthebasisofaninitialreservoircontentof1.00MMSCFofwetgas,calculatethe wetgas,residuegas,andcondensaterecoverybypressuredepletionforeachpressure interval. (b) Calculatethedrygasandcondensateinitiallyinplacein1.00MMSCFofwetgas. (c) Calculatethecumulativerecoveryandthepercentageofrecoveryofwetgas,residue gas,andcondensatebydepletionperformanceateachpressure. (d) Calculatetherecoveriesatanabandonmentpressureof605psiaonanacre-footbasis foraporosityof10%andaconnatewaterof20%. Composition in mole percentages Pressure (psia) 4000 3500 2900 2100 1300 605 CO2 0.18 0.18 0.18 0.18 0.19 0.21 N2 0.13 0.13 0.14 0.15 0.15 0.14 C1 67.72 63.10 65.21 69.79 70.77 66.59 C2 14.10 14.27 14.10 14.12 14.63 16.06 Problems 155 Composition in mole percentages Pressure (psia) 4000 3500 2900 2100 1300 605 C3 8.37 8.25 8.10 7.57 7.73 9.11 iC4 0.98 0.91 0.95 0.81 0.79 1.01 nC4 3.45 3.40 3.16 2.71 2.59 3.31 iC5 0.91 0.86 0.84 0.67 0.55 0.68 nC5 1.52 1.40 1.39 0.97 0.81 1.02 C6 1.79 1.60 1.52 1.03 0.73 0.80 C7+ 6.85 5.90 4.41 2.00 1.06 1.07 Molecular weightC7+ 143 138 128 116 111 110 Gas deviation factorfor wetgasat 186°F 0.867 0.799 0.748 0.762 0.819 0.902 Wetgas production (cm3)at cellP and T 0 224.0 474.0 1303 2600 5198 Wetgas GPM (calculated) 5.254 4.578 3.347 1.553 0.835 0.895 Residue gas-oilratio 7127 8283 11,621 26,051 49,312 45,872 Retrograde liquid, percentage ofcell volume 0 3.32 19.36 23.91 22.46 18.07 5.9 IftheretrogradeliquidforthereservoirofProblem5.8becomesmobileat15%retrograde liquidsaturation,whateffectwillthishaveonthecondensaterecovery? 5.10 IftheinitialpressureofthereservoirofProblem5.8hadbeen5713psiawiththedewpoint at4000psia,calculatetheadditionalrecoveryofwetgas,residuegas,andcondensateper acre-foot.Thegasdeviationfactorat5713psiais1.107,andtheGPMandGORbetween 5713and4000psiaarethesameasat4000psia. Chapter 5 156 • Gas-Condensate Reservoirs 5.11 CalculatethevalueoftheproductsbyeachmechanisminTable5.8assuming(1)$85.00 perSTBforcondensateand$5.50perMSCFforgas;(2)$95.00perSTBand$6.00perM SCF;and(3)$95.00perSTBand$6.50perMSCF. 5.12 InaPVTstudyofagas-condensatefluid,17.5cm3ofwetgas(vapor),measuredatcellpressureof2500psiaandtemperatureof195°F,wasdisplacedintoanevacuatedlow-pressure receiverof5000cm3volumethatwasmaintainedat250°Ftoensurethatnoliquidphase developedintheexpansion.Ifthepressureofthereceiverrisesto620mmHg,whatwill bethedeviationfactorofthegasinthecellat2500psiaand195°F,assumingthegasinthe receiverbehavesideally? 5.13 UsingtheassumptionsofExample5.3andthedataofTable5.3,showthatthecondensate recovery between 2000 and 1500 psia is 14.0 STB/ac-ft and the residue gas-oil ratio is 19,010SCF/bbl. 5.14 Astock-tankbarrelofcondensatehasagravityof55°API.Estimatethevolumeinft3occupiedbythiscondensateasasingle-phasegasinareservoirat2740psiaand215°F.The reservoirwetgashasagravityof0.76. 5.15 Agas-condensatereservoirhasanarealextentof200acres,anaveragethicknessof15ft, anaverageporosityof0.18,andaninitialwatersaturationof0.23.APVTcellisusedto simulatetheproductionfromthereservoir,andthefollowingdataarecollected: Pressure (psia) Wet gas produced (cc) z wet gas Condensate produced from separator (moles) 4000(dewpoint) 0 0.75 0 3700 400 0.77 0.0003 3300 450 0.81 0.0002 Theinitialcellvolumewas1850cc,andtheinitialgascontained0.002molsofcondensate.Theinitialpressureis4000psia,andthereservoirtemperatureis200°F.Calculatetheamountofdrygas(SCF)andcondensate(STB)recoveredat3300psiafromthe reservoir.Themolecularweightandspecificgravityofthecondensateare145and0.8, respectively. 5.16 Production from a gas-condensate reservoir is listed below. The molecular weight and thespecificgravityofthecondensateare150and0.8,respectively.Theinitialwetgasin placewas35MMMSCF,andtheinitialcondensatewas2MMSTB.Assumeavolumetric reservoirandthattherecoveriesofcondensateandwaterareidentical,anddeterminethe following: References 157 (a) Whatisthepercentageofrecoveryofresiduegasat3300psia? (b) Can a PVT cell experiment be used to simulate the production from this reservoir? Whyorwhynot? Pressure(psia) 4000 3500 3300 Compressibilityofwetgas(z) 0.85 0.80 0.83 Wetgasproducedduringpressure increment(SCF) 0 2.4MMM 2.2MMM Liquidcondensateproducedduring pressureincrement(STB) 0 80,000 70,000 Waterproducedduringpressureincrement (STB) 0 5000 4375 5.17 APVTcellisusedtosimulateagas-condensatereservoir.Theinitialcellvolumeis1500cc, andtheinitialreservoirtemperatureis175°F.ShowbycalculationsthatthePVTcellwillor willnotadequatelysimulatethereservoirbehavior.ThedatageneratedbythePVTexperimentsaswellastheactualproductionhistoryareasfollows: Pressure(psia) Wetgasproducedinpressureincrement(cc) Compressibilityofproducedgas Actualproductionhistory(MSCF) 4000 3600 3000 0 300 700 0.70 0.73 0.77 0 1000 2300 References 1. J.C.Allen,“FactorsAffectingtheClassificationofOilandGasWells,”API Drilling and Production Practice(1952),118. 2. Ira Rinehart’s Yearbooks,Vol.2,RinehartOilNews,1953–57. 3. M.Muskat,Physical Principles of Oil Production,McGraw-Hill,1949,Chap.15. 4. M.B.Standing,Volumetric and Phase Behavior of Oil Field Hydrocarbon Systems,Reinhold Publishing,1952,Chap.6. 5. O.F.Thornton,“Gas-CondensateReservoirs—AReview,”API Drilling and Production Practice(1946),150. 6. C.K.Eilerts,Phase Relations of Gas-Condensate Fluids,Vol.1,Monograph10,USBureau ofMines,AmericanGasAssociation,1957. 7. T. A. Mathews, C. H. Roland, and D. L. Katz, “High Pressure Gas Measurement,” Proc. NGAA(1942),41. 158 Chapter 5 • Gas-Condensate Reservoirs 8. J.K.Rodgers,N.H.Harrison,andS.Regier,“ComparisonbetweenthePredictedandActual ProductionHistoryofaCondensateReservoir,”paper883-G,presentedattheAlMEmeeting, Oct.1957,Dallas,TX. 9. W.E.PortmanandJ.M.Campbell,“EffectofPressure,Temperature,andWell-StreamCompositionontheQuantityofStabilizedSeparatorFluid,”Trans.AlME(1956),207,308. 10. R.L.Huntington,Natural Gas and Natural Gasoline,McGraw-Hill,1950,Chap.7. 11. Natural Gasoline Supply Men’s Association Engineering Data Book,7thed.,NaturalGasoline SupplyMen’sAssociation,1957,161. 12. A.E.Hoffmann,J.S.Crump,andC.R.Hocott,“EquilibriumConstantsforaGas-Condensate System,”Trans.AlME(1953),198,1. 13. F.H.AllenandR.P.Roe,“PerformanceCharacteristicsofaVolumetricCondensateReservoir,”Trans.AlME(1950),189,83. 14. J.E.Berryman,“ThePredictedPerformanceofaGas-CondensateSystem,WashingtonField, Louisiana,”Trans.AlME(1957),210,102. 15. R.H.Jacoby,R.C.Koeller,andV.J.BerryJr.,“EffectofCompositionandTemperatureon PhaseBehaviorandDepletionPerformanceofGas-CondensateSystems,”paperpresentedat theAnnualConferenceofSPEofAlME,Oct.5–8,1958,Houston,TX. 16. C. W. Donohoe and R. D. Buchanan, “Economic Evaluation of Cycling Gas-Condensate ReservoirswithNitrogen,”Jour. of Petroleum Technology(Feb.1981),263. 17. P. L. Moses and K.Wilson, “Phase Equilibrium Considerations in Using Nitrogen for Improved Recovery from Retrograde Condensate Reservoirs,” Jour. of Petroleum Technology (Feb.1981),256. 18. J.L.VogelandL.Yarborough,“TheEffectofNitrogenonthePhaseBehaviorandPhysical PropertiesofReservoirFluids,”paperSPE8815,presentedattheFirstJointSPE/DOESymposiumonEnhancedOilRecovery,Apr.1980,Tulsa,OK. 19. P.M.Sigmund,“PredictionofMolecularDiffusionatReservoirConditions.PartI—Measurement andPredictionofBinaryDenseGasDiffusionCoefficients,”Jour. of Canadian Petroleum Technology(Apr.–June1976),48. 20. P.M.Sigmund,“PredictionofMolecularDiffusionofReservoirConditions.PartII—Estimating theEffectsofMolecularDiffusionandConvectiveMixinginMulti-ComponentSystems,”Jour. of Canadian Petroleum Technology(July–Sept.1976),53. 21. S.W.Kleinsteiber,D.D.Wendschlag,andJ.W.Calvin,“AStudyforDevelopmentofaPlan ofDepletioninaRichGasCondensateReservoir:AnschutzRanchEastUnit,SummitCounty, Utah,UintaCounty,Wyoming,”paperSPE12042,presentedatthe58thAnnualConferenceof SPEofAlME,Oct.1983,SanFrancisco. 22. L. Yarborough, “Application of a Generalized Equation of State to Petroleum Reservoir Fluids,”Equations of State in Engineering, Advances in Chemical Series,ed.K.C.Chaoand R.L.Robinson,AmericanChemicalSociety,1979,385. C H A P T E R 6 Undersaturated Oil Reservoirs 6.1 Introduction Atthebeginningofthistext,thevarioushydrocarbonreservoirsweresubdividedintofourtypes. Thischaptercontainsadiscussiononreservoirsthathaveonlyliquidphasesinitiallypresent.The nextchapterwillconsideroilreservoirsthathaveaninitialgascap.Thesetworeservoirtypesdiffer significantlyfromthegasreservoirs.Thedifferencesstemfromthecompositionofthereservoir fluidsandresultinadistinctprimaryproductionmethod—thatofdepletiondrive.Comparedto volumetric gas drive, depletion drive is a weaker primary production method and more factors, suchasrockandwatercompressibility,mustbeconsideredinordertoaccuratelypredictthebehaviorofthereservoir.Thesamemethod,thematerialbalance,willbeusedinthisprediction;it will,however,requireadditionalterms. Oilinplaceforoilreservoirscanbecalculatedintwoways.Ifavailable,wellandseismic datacanbeusedtocalculatetheoilinplaceusingtechniqueslikethoseexplainedinChapter4. Alternately,oilandgasproductiondatacombinedwithpressureandsaturationdatacanbeusedin amaterialbalanceemployingequationsfromChapter3. 6.1.1 Oil Reservoir Fluids Oilreservoirfluidsaremainlycomplexmixturesofthehydrocarboncompounds,whichfrequently contain impurities such as nitrogen, carbon dioxide, and hydrogen sulfide. The composition in molepercentagesofseveraltypicalreservoirliquidsisgiveninTable6.1,togetherwiththetank gravityofthecrudeoil,thegas-oilratioofthereservoirmixture,andothercharacteristicsofthe fluids.1Thecompositionofthetankoilsobtainedfromthereservoirfluidsarequitedifferentfrom thecompositionofthereservoirfluids,owingmainlytothereleaseofmostofthemethaneand ethanefromsolutionandthevaporizationofsizeablefractionsofthepropane,butanes,andpentanes,aspressureisreducedinpassingfromthereservoirtothestocktank.Thetableshowsagood correlationbetweenthegas-oilratiosofthefluidsandthepercentagesofmethaneandethanethey containoverarangeofgas-oilratios,fromonly22SCF/STBupto4053SCF/STB. 159 Chapter 6 160 • Undersaturated Oil Reservoirs Table 6.1 Reservoir Fluid Compositions and Properties (after Kennerly, Courtesy Core Laboratories, Inc.)1 Component California or property Wyoming South Texas North Texas West Texas South Louisiana Methane 22.62 1.08 48.04 25.63 28.63 65.01 Ethane 1.69 2.41 3.36 5.26 10.75 7.84 Propane 0.81 2.86 1.94 10.36 9.95 6.42 iso-Butane 0.51 0.86 0.43 1.84 4.36 2.14 n-Butane 0.38 2.83 0.75 5.67 4.16 2.91 iso-Pentane 0.19 1.68 0.78 3.14 2.03 1.65 n-Pentane 0.19 2.17 0.73 1.91 3.83 0.83 Hexanes 0.62 4.51 2.79 4.26 2.35 1.19 Heptanes-plus 72.99 81.60 41.18 41.93 33.94 12.01 Density heptanes-plus (g/cc) 0.957 0.920 0.860 0.843 0.792 0.814 Molecular weight, heptanes-plus 360 289 198 231 177 177 Sampling depth(ft) 2980 3160 8010 4520 12,400 10,600 Reservoir temperature (°F) 141 108 210 140 202 241 Saturation pressure (psig) 1217 95 3660 1205 1822 4730 GOR(SCF/ STB) 105 22 750 480 895 4053 Formation volumefactor (bbl/STB) 1.065 1.031 1.428 1.305 1.659 3.610 Tank oil gravity (°API) 16.3 25.1 34.8 40.6 50.8 43.5 Gasgravity (air=1.00) 0.669 ... 0.715 1.032 1.151 0.880 6.1 Introduction 161 Severalmethodsareavailableforcollectingsamplesofreservoirfluids.Thesamplesmaybe takenwithsubsurfacesamplingequipmentloweredintothewellonawireline,orsamplesofthe gasandoilmaybecollectedatthesurfaceandlaterrecombinedinproportiontothegas-oilratio measuredatthetimeofsampling.Samplesshouldbeobtainedasearlyaspossibleinthelifeofthe reservoir,preferablyatthecompletionofthediscoverywell,sothatthesampleapproachesasnearly aspossibletheoriginalreservoirfluid.Thetypeoffluidcollectedinasamplerisdependentonthe wellhistorypriortosampling.Unlessthewellhasbeenproperlyconditionedbeforesampling,it isimpossibletocollectrepresentativesamplesofthereservoirfluid.Acompletewell-conditioning procedurehasbeendescribedbyKennedyandReudelhuber.1,2Theinformationobtainedfromthe usualfluidsampleanalysisincludesthefollowingproperties: 1. Solutionandevolvedgas-oilratiosandliquidphasevolumes 2. Formationvolumefactors,tankoilgravities,andseparatorandstock-tankgas-oilratiosfor variousseparatorpressures 3. Bubble-pointpressureofthereservoirfluid 4. Compressibilityofthesaturatedreservoiroil 5. Viscosityofthereservoiroilasafunctionofpressure 6. Fractionalanalysisofacasingheadgassampleandofthesaturatedreservoirfluid Iflaboratorydataarenotavailable,satisfactoryestimationsforapreliminaryanalysiscanoftenbe madefromempiricalcorrelations,likethoseconsideredinChapter2,thatarebasedondatausually available.Thesedataincludethegravityofthetankoil,thespecificgravityoftheproducedgas, theinitialproducinggas-oilratio,theviscosityofthetankoil,thereservoirtemperature,andthe initialreservoirpressure. Inmostreservoirs,thevariationsinthereservoirfluidpropertiesamongsamplestakenfrom differentportionsofthereservoirarenotlarge,andtheyliewithinthevariationsinherentinthe techniquesoffluidsamplingandanalysis.Insomereservoirs,ontheotherhand,particularlythose withlargeclosures,therearelargevariationsinthefluidproperties.Forexample,intheElkBasinField,WyomingandMontana,underinitialreservoirconditions,therewas490SCFofgasin solutionperbarrelofoilinasampletakennearthecrestofthestructurebutonly134SCF/STB inasampletakenontheflanksofthefield,1762ftlowerinelevation.3Thisisasolutiongasgradientof20SCF/STBper100ftofelevation.Becausethequantityofsolutiongashasalargeeffect ontheotherfluidproperties,largevariationsalsooccurinthefluidviscosity,theformationvolume factor,andthelike.SimilarvariationshavebeenreportedfortheWebersandstonereservoirofthe RangelyField,Colorado,andtheScurryReefField,Texas,wherethesolutiongasgradientswere 25 and 46 SCF/STB per 100 ft of elevation, respectively.4,5These variations in fluid properties maybeexplainedbyacombinationof(1)temperaturegradients,(2)gravitationalsegregation,and (3)lackofequilibriumbetweentheoilandthesolutiongas.Cook,Spencer,Bobrowski,andChin, andMcCordhavepresentedmethodsforhandlingcalculationswhentherearesignificantvariationsinthefluidproperties.5,6 Chapter 6 162 • Undersaturated Oil Reservoirs 6.2 Calculating Oil in Place and Oil Recoveries Using Geological, Geophysical, and Fluid Property Data Oneoftheimportantfunctionsofthereservoirengineeristheperiodiccalculationofthereservoir oil(andgas)inplaceandtherecoveryanticipatedundertheprevailingreservoirmechanism(s).In somecompanies,thisworkisdonebyagroupthatperiodicallyrendersanaccountofthecompany’sreservestogetherwiththeratesatwhichtheycanberecoveredinthefuture.Thecompany’s financialpositiondependsprimarilyonitsreserves,therateatwhichitincreasesorlosesthem,and theratesatwhichtheycanberecovered.Aknowledgeofthereservesandratesofrecoveryisalso importantinthesaleorexchangeofoilproperties.Thecalculationofreservesofnewdiscoveries isparticularlyimportantbecauseitservesasaguidetosounddevelopmentprograms.Likewise,an accurateknowledgeoftheinitialcontentsofreservoirsisinvaluabletothereservoirengineerwho studiesthereservoirbehaviorwiththeaimofcalculatingand/orimprovingprimaryrecoveries— foriteliminatesoneoftheunknownquantitiesinequations. Oilreservesareusuallyobtainedbymultiplyingtheoilinplacebyarecoveryfactor,where the recovery factor is the estimated fraction of the oil in place that will be produced through a particularproductionorreservoirdrivemechanism.Theycanalsobeestimatedfromdeclinecurve studiesandbyapplyingappropriatebarrel-per-acre-footrecoveryfiguresobtainedfromexperience orstatisticalstudiesofwellorreservoirproductiondata.Theoilinplaceiscalculatedeither(1)by theuseofgeological,geophysical,andfluidpropertydataor(2)bymaterialbalancestudies,both ofwhichwerepresentedforgasreservoirsinChapter4andwillbegivenforoilreservoirsinthis andfollowingchapters.Inthelattercase,recoveryfactorsaredeterminedfrom(1)displacement efficiencystudiesand(2)correlationsbasedonstatisticalstudiesofparticulartypesofreservoir mechanisms. The first method for estimating oil in place starts with an estimate of the bulk reservoir volumeusingthetechniquesconsideredinChapter4.Thenlogandcoreanalysisdataareusedto determinethebulkvolume,porosity,andfluidsaturations,andfluidanalysisdataareusedtodeterminetheoilvolumefactor.Underinitialconditions,1ac-ftofbulkoilproductiverockcontains thefollowing: Interstitialwater=7758× φ × Sw Reservoiroil=7758× φ ×(1–Sw) Stock-tankoil= 7758 × φ × (1 − Sw ) Boi where7758barrelsistheequivalentof1ac-ft, φistheporosityasafractionofthebulkvolume, Swistheinterstitialwaterasafractionoftheporevolume,andBoiistheinitialformationvolume factorofthereservoiroil.Usingsomewhataveragevalues(φ=0.20,Sw=0.20,andBoi=1.24),the initialstock-tankoilinplaceperacre-footisontheorderof1000STB/ac-ft,or 6.2 Calculating Oil in Place and Oil Recoveries Stock-tankoil= 163 7785 × 0.20 × (1 − 0.20 ) 1.24 =1000STB/ac-ft Foroilreservoirsundervolumetric control,thereisnowaterinfluxtoreplacetheproduced oil,soitmustbereplacedbytheswellingoftheoilphaseorexpandinggas,thesaturationofwhich increasesastheoilsaturationdecreases.IfSgisthegassaturationandBotheoilvolumefactorat abandonment,thenatabandonmentconditions,1ac-ftofbulkrockcontainsthefollowing: Interstitialwater=7758× φ × Sw Reservoirgas=7758× φ × Sg Reservoiroil=7758× φ ×(1–Sw – Sg) Stock-tankoil= 7758 × φ × (1 − Sw − Sg ) Bo Thentherecoveryinstock-tankbarrelsperacre-footis (1 − Sw ) (1 − Sw − Sg ) − Recovery=7758× φ Bo Boi (6.1) andthefractionalrecoveryintermsofstock-tankbarrelsis Fractionalrecovery=1– (1 − Sw − Sg ) (1 − Sw ) × Boi Bo (6.2) Thetotalfreegassaturationtobeexpectedatabandonmentcanbeestimatedfromtheoilandwater saturationsasreportedincoreanalysis.7Thisexpectationisbasedontheassumptionthat,while beingremovedfromthewell,thecoreissubjectedtofluidremovalbytheexpansionofthegas liberatedfromtheresidualoilandthatthisprocessissomewhatsimilartothedepletionprocessin thereservoir.Inastudyofthewell-spacingproblem,CrazeandBuckleycollectedalargeamount ofstatisticaldataon103oilreservoirs,27ofwhichwereconsideredtobeproducingundervolumetriccontrol.8,9Thefinalgassaturationinmostofthesereservoirsrangedfrom20%to40%ofthe porespace,withanaveragesaturationof30.4%.Recoveriesmayalsobecalculatedfordepletion performancefromaknowledgeofthepropertiesofthereservoirrockandfluids. Inthecaseofreservoirsunderhydraulic control,wherethereisnoappreciabledeclinein reservoirpressure,waterinfluxiseitherinwardandparalleltothebeddingplanes,asfoundinthin, Chapter 6 164 • Undersaturated Oil Reservoirs relativelysteepdippingbeds(edgewaterdrive),orupwardwheretheproducingoilzone(column) isunderlainbywater(bottomwaterdrive).Theoilremainingatabandonmentinthoseportionsof thereservoirinvadedbywater,inbarrelsperacre-foot,isasfollows: Reservoiroil=7758× φ × Sor Stock-tankoil= 7758 × φ × Sor Boi whereSoristheresidualoilsaturationremainingafterwaterdisplacement.Sinceitwasassumed thatthereservoirpressurewasmaintainedatitsinitialvaluebythewaterinflux,nofreegassaturationdevelopsintheoilzone,andtheoilvolumefactoratabandonmentremainsBoi.Therecovery byactivewaterdrivethenis Recovery= 7758 × φ (1 − Sw − Sor ) STB/ac-ft Boi (6.3) (1 − Sw − Sor ) (1 − Sw ) (6.4) andtherecoveryfactoris Recovery= Itisgenerallybelievedthattheoilcontentofcores,reportedfromtheanalysisofcorestaken withawater-baseddrillingfluid,isareasonableestimationoftheunrecoverableoilbecausethe core has been subjected to a partial water displacement (by the mud filtrate) during coring and to displacement by the expansion of the solution gas as the pressure on the core is reduced to atmosphericpressure.10IfthisfigureisusedfortheresidentoilsaturationinEqs.(6.3)and(6.4), itshouldbeincreasedbytheformationvolumefactor.Forexample,aresidualoilsaturationof 20%fromcoreanalysisindicatesaresidualreservoirsaturationof30%foranoilvolumefactorof 1.50bbl/STB.TheresidualoilsaturationmayalsobeestimatedusingthedataofTable4.2,which shouldbeapplicabletoresidualoilsaturationsaswellasgassaturations(i.e.,intherangeof25% to40%fortheconsolidatedsandstonesstudied). InthereservoiranalysismadebyCrazeandBuckley,some70ofthe103fieldsanalyzed producedwhollyorpartiallyunderwater-driveconditions,andtheresidualoilsaturationsranged from17.9%to60.9%oftheporespace.8AccordingtoArps,thedataapparentlyrelateaccordingto thereservoiroilviscosityandpermeability.7Theaveragecorrelationbetweenoilviscosityandresidualoilsaturation,bothunderreservoirconditions,isshowninTable6.2.AlsoincludedinTable 6.2isthedeviationofthistrendagainstaverageformationpermeability.Forexample,theresidual oilsaturationunderreservoirconditionsforaformationcontaining2cpoilandhavinganaverage permeabilityof500mdisestimatedat37+2,or39%oftheporespace. 6.2 Calculating Oil in Place and Oil Recoveries 165 Table 6.2 Correlation between Reservoir Oil Viscosity, Average Reservoir Permeability, and Residual Oil Saturation (after Craze and Buckley and Arps)7,8 Reservoir oil viscosity (in cp) Residual oil saturation (percentage of pore space) 0.2 30 0.5 32 1.0 34.5 2.0 37 5.0 40.5 10.0 43.5 20.0 64.5 Average reservoir permeability (in md) Deviation of residual oil saturation from viscosity trend (percentage of pore space) 50 +12 100 +9 200 +6 500 +2 1000 –1 2000 –4.5 5000 –8.5 BecauseCrazeandBuckley’sdatawerearrivedatbycomparingrecoveriesfromthereservoirasawholewiththeestimatedinitialcontent,theresidualoilcalculatedbythismethodincludes asweepefficiencyaswellastheresidualoilsaturation—thatis,thefiguresarehigherthanthe residualoilsaturationsinthoseportionsofthereservoirinvadedbywateratabandonment.This sweepefficiencyreflectstheeffectofwelllocation,thebypassingofsomeoftheoilintheless permeablestrata,andtheabandonmentofsomeleasesbeforethefloodingactioninallzonesis complete,owingtoexcessivewater-oilratios,inbothedgewaterandbottomwaterdrives. InastatisticalstudyofCrazeandBuckley’swater-driverecoverydata,GuthrieandGreenberger, using multiple correlation analysis methods, found the following correlation between water-driverecoveryandfivevariablesthataffectrecoveryinsandstone reservoirs.11 RF=0.114+0.272logk+0.256Sw–0.136logμo–1.5384φ–0.00035h Fork=1000md,Sw=0.25,μo =2.0cp,φ=0.20,andh=10ft, RF=0.114+0.272×log1000+0.256×0.25–0.136 log2–1.538×0.20–0.00035×10 (6.5) Chapter 6 166 where • Undersaturated Oil Reservoirs 0.642,or64.2%(ofinitialstock-tankoil) RF = recovery factor Atestoftheequationshowedthat50%ofthefieldshadrecoverieswithin± 6.2%recoveryofthat predictedbyEq.(6.5),75%werewithin± 9.0%recovery,and100%werewithin±19.0%recovery.Forinstance,itis75%probablethattherecoveryfromtheforegoingexampleis64.2±9.0%. Although it is usually possible to determine a reasonably accurate recovery factor for a reservoirasawhole,thefiguremaybewhollyunrealisticwhenappliedtoaparticularleaseor portionofareservoir,owingtotheproblemoffluidmigrationinthereservoir,alsoreferredtoas lease drainage.Forexample,aflankleaseinawater-drivereservoirmayhave50,000STBofrecoverablestock-tankoilinplacebutwilldivideitsreservewithallupdipwellsinlinewithit.The degreetowhichmigrationmayaffecttheultimaterecoveriesfromvariousleasesisillustratedin Fig.6.1.12Ifthewellsarelocatedon40-acreunits,ifeachwellhasthesamedailyallowable,if thereisuniformpermeability,andifthereservoirisunderanactivewaterdrivesothatthewater B C D E F W at er Oi l A Figure 6.1 Effect of water drive on oil migration (after Buckley, AlME).12 G 6.3 Material Balance in Undersaturated Reservoirs 167 advancesalongahorizontalsurface,thentherecoveryfromleaseAisonlyone-seventhofthe recoverableoilinplace,whereasleaseGrecoversone-seventhoftherecoverableoilunderlease A,one-sixthunderleaseB,one-fifthunderleaseC,andsoon.Leasedrainageisgenerallyless severewithotherreservoirmechanisms,butitoccurstosomeextentinallreservoirs. 6.3 Material Balance in Undersaturated Reservoirs ThematerialbalanceequationforundersaturatedreservoirswasdevelopedinChapter3: cw Swi + c f N(Bt – Bti)+NBti 1 − Swi Δ p + We = Np[Bt+(Rp – Rsoi)Bg] + BwWp (3.8) Neglectingthechangeinporosityofrockswiththechangeofinternalfluidpressure,whichis treatedlater,reservoirswithzeroornegligiblewaterinfluxareconstantvolumeorvolumetric reservoirs.Ifthereservoiroilisinitiallyundersaturated,theninitiallyitcontainsonlyconnate water and oil, with their solution gas. The solubility of gas in reservoir waters is generally quitelowandisconsiderednegligibleforthepresentdiscussion.Becausethewaterproduction from volumetric reservoirs is generally small or negligible, it will be considered zero. From initialreservoirpressuredowntothebubblepoint,then,thereservoiroilvolumeremainsaconstant,andoilisproducedbyliquidexpansion.IncorporatingtheseassumptionsintoEq.(3.8), thefollowingisobtained: N(Bt – Bti)=Np[Bt+(Rp – Rsoi)Bg] (6.6) While the reservoir pressure is maintained above the bubble-point pressure and the oil remains undersaturated,onlyliquidwillexistinthereservoir.Anygasthatisproducedonthesurfacewill begascomingoutofsolutionastheoilmovesupthroughthewellboreandthroughthesurface facilities.Allthisgaswillbegasthatwasinsolutionatreservoirconditions.Therefore,duringthis period, RpwillequalRso and RsowillequalRsoi,sincethesolutiongas-oilratioremainsconstant(see Chapter2).Thematerialbalanceequationbecomes N(Bt – Bti) = NpBt (6.7) Thiscanberearrangedtoyieldfractionalrecovery,RF, as RF = Np N = Bt − Bti Bt (6.8) Thefractionalrecoveryisgenerallyexpressedasafractionoftheinitialstock-tankoilinplace. Thepressure-volume-temperature(PVT)dataforthe3–A–2reservoirofafieldisgiveninFig.6.2. Chapter 6 168 • Undersaturated Oil Reservoirs 1.65 1100 0.90 rm 1.40 D e v i a ti o n fa c 900 800 700 600 0.88 t or 500 0.86 1.35 1.30 800 Gas deviation factor fa c e 0.92 at io n- vo lu m il -o s Ga 1.45 to io r 1.50 0.94 Solution gas-oil ratio, SCF/STB Original saturation pressure 1.55 t ra 1000 0.96 Fo Formation volume factor, bbl/STB 1.60 400 300 1200 1600 2000 2400 2800 3200 3600 4000 4400 Pressure, psia Figure 6.2 PVT data for the 3–A–2 reservoir at 190°F. TheformationvolumefactorplottedinFig.6.2isthesingle-phaseformationvolumefactor, Bo.Thematerialbalanceequationhasbeenderivedusingthetwo-phaseformationvolumefactor, Bt. Bo and BtarerelatedbyEq.(2.29): Bt = Bo + Bg(Rsoi – Rso) (2.29) ItshouldbeapparentthatBt = Boabovethebubble-pointpressurebecauseRso isconstantand equaltoRsoi. Thereservoirfluidhasanoilvolumefactorof1.572bbl/STBattheinitialpressure4400psia and1.600bbl/STBatthebubble-pointpressureof3550psia.Then,byvolumetricdepletion,the fractionalrecoveryofthestock-tankoilat3550psiabyEq.(6.8)is RF = 1.600 − 1.572 = 0.0175 or1.75% 1.600 Ifthereservoirproduced680,000STBwhenthepressuredroppedat3550psia,thentheinitialoil inplacebyEq.(6.7)is N= 1.600 × 680, 000 = 38.8 MMSTB 1.600 − 1.572 6.3 Material Balance in Undersaturated Reservoirs 169 Below3550psia,afree gasphasedevelops;andforavolumetric,undersaturatedreservoir withnowaterproduction,thehydrocarbonporevolumeremainsconstant,or Voi = Vo + Vg (6.9) Figure6.3showsschematicallythechangesthatoccurbetweeninitialreservoirpressureandsome pressurebelowthebubblepoint.Thefree-gasphasedoesnotnecessarilyrisetoformanartificial gascap,andtheequationsarethesameifthe free gasremainsdistributedthroughoutthereservoir asisolatedbubbles.Equation(6.6)canberearrangedtosolveforNandthefractionalrecovery,RF, foranyundersaturatedreservoirbelowthebubblepoint. N= RF = N p [ Bt + ( Rp − Rsoi ) Bg ] (6.10) ( Bt − Bti ) Np N = ( Bt − Bti ) [ Bt + ( R p − Rsoi ) Bg ] (6.11) Thenet cumulative produced gas-oil ratio (Rp)isthequotientofallthegasproducedfromthereservoir(Gp)andalltheoilproduced(Np).Insomereservoirs,someoftheproducedgasisreturned tothesamereservoir,sothatthenetproducedgasisonlythatwhichisnotreturnedtothereservoir. Whenalltheproducedgasisreturnedtothereservoir,Rpiszero. AninspectionofEq.(6.11)indicatesthatallthetermsexcepttheproducedgas-oilratio(Rp) arefunctionsofpressureonlyandarethepropertiesofthereservoirfluid.Becausethenatureofthe fluidisfixed,itfollowsthatthefractionalrecoveryRFisfixedbythePVTpropertiesofthereservoirfluidandtheproducedgas-oilratio.Sincetheproducedgas-oilratiooccursinthedenominator ofEq.(6.11),largegas-oilratiosgivelowrecoveriesandviceversa. Production Np STB and Np Rp SCF Free gas (N – NP) STB + (N – NP) RS SCF N STB + N RSI SCF PB Figure 6.3 P Diagram showing the formation of a free-gas phase in a volumetric reservoir below the bubble point. Chapter 6 170 Example 6.1 • Undersaturated Oil Reservoirs Calculating the Effect of the Produced Gas-Oil Ratio (Rp) on Fractional Recovery in Volumetric, Undersaturated Reservoirs Given ThePVTdataforthe3–A–2reservoir(Fig.6.2) CumulativeGORat2800psia=3300SCF/STB Reservoirtemperature=190°F=650°R Standardconditions=14.7psiaand60°F Solution The following values are determined graphically from Fig 6.2. RsoiistheGORattheinitialreservoirconditionofp=4400psiaandRsoi=1100SCF/STB.Boi istheformationvolumefactorat initialreservoirconditionsofp=4400psiaand Boi=1.572bbl/STB.At2800psia,Rso istheGOR at900SCF/STBandBo istheformationvolumefactorat1.520bbl/STB.Rp wasgivenasthe cumulativeGORat2800psia.Bg and Btat2800psiaarecalculatedasfollowsfromEqs.(2.16) and(2.29): Bg = 0.00504 (0.87)650 zT = 0.00504 = 0.00102 bbl/SCF 2800 p Bt = Bo + Bg(Rsoi – Rso) Bt=1.520+0.00102(1100–900)=1.724bbl/STB Then,usingEq.(6.11)at2800psia, RF = 1.724 − 1.572 1.724+0.00102(3300 − 1100) =0.0383,or3.83% Iftwo-thirdsoftheproducedgashadbeenreturnedtothereservoir,atthesamepressure(i.e., 2800psia), Rp wouldbe1100SCF/STBandthefractionalrecoverywouldhavebeen RF = 1.724 − 1.572 1.724+0.00102(1100 − 1100) =0.088,or8.8% 6.4 Kelly-Snyder Field, Canyon Reef Reservoir 171 Equation(6.10)maybeusedtofindtheinitialoilinplace.Forexample,if1.486MMSTBhad beenproduceddownto2800psia,forRp=3300SCF/STB,theinitialoilinplaceis N= 1.486 × 10 6 [1.724 + 0.00102( 3300 − 1100 )] 1.724 − 1.572 =38.8MMSTB ThecalculationsofExample6.1forthe3–A–2reservoirshowthat,forRp=3300SCF/STB,the recoveryat2800psiais3.83%andthat,ifRphadbeenonly1100SCF/STB,therecoverywould havebeen8.80%.Neglectingineachcasethe1.75%recoverybyliquidexpansiondowntothe bubble-pointpressure,theeffectofreducingthegas-oilratiobyone-thirdisapproximatelytotripletherecovery.Theproducedgas-oilratiocanbecontrolledbyworkingoverhighgas-oilratio wells,byshuttinginorreducingtheproducingratesofhighratiowells,and/orbyreturningsome oralloftheproducedgastothereservoir.Ifgravitationalsegregationoccursduringproduction sothatagascapforms,asshowninFig.6.3,andiftheproducingwellsarecompletedlowin theformation,theirgas-oilratioswillbelowerandrecoverywillbeimproved.Simplyfromthe materialbalancepointofview,byreturningallproducedgastothereservoir,itispossibleto obtain100%recoveries.Fromthepointofviewofflowdynamics,however,apracticallimitis reachedwhenthereservoirgassaturationrisestovaluesintherangeof10%to40%because thereservoirbecomessopermeabletogasthatthereturnedgasmovesrapidlyfromtheinjectionwellstotheproductionwells,displacingwithitonlyasmallquantityofoil.Thusalthough gas-oilratiocontrolisimportantinsolutiongas-drivereservoirs,recoveriesareinherentlylow becausethegasisproducedfasterthantheoil.Outsidetheenergystoredupintheliquidabove thebubblepoint,theenergyforproducingtheoilisstoredupinthesolutiongas.Whenthisgas hasbeenproduced,theonlyremainingnaturalsourceofenergyisgravitydrainage,andthere maybeaconsiderableperiodinwhichtheoildrainsdownwardtothewellsfromwhichitis pumpedtothesurface. Inthenextsection,amethodispresentedthatallowsthematerialbalanceequationtobeused asapredictivetool.ThemethodwasusedbyengineersperformingcalculationsontheCanyon ReefReservoirintheKelly-SnyderField. 6.4 Kelly-Snyder Field, Canyon Reef Reservoir TheCanyonReefreservoiroftheKelly-SnyderField,Texas,wasdiscoveredin1948.During theearlyyearsofproduction,therewasmuchconcernabouttheveryrapiddeclineinreservoir pressure;however,reservoirengineerswereabletoshowthatthiswastobeexpectedofavolumetricundersaturatedreservoirwithaninitialpressureof3112psigandabubble-pointpressure ofonly1725psig,bothatadatumof4300ftsubsea.13Theircalculationsfurthershowedthat whenthebubble-pointpressureisreached,thepressuredeclineshouldbemuchlessrapid,and that the reservoir could be produced without pressure maintenance for many years thereafter Chapter 6 172 • Undersaturated Oil Reservoirs without prejudice to the pressure maintenance program eventually adopted. In the meantime, with additional pressure drop and production, further reservoir studies could evaluate the potentialitiesofwaterinflux,gravitydrainage,andintrareservoircommunication.These,together withlaboratorystudiesoncorestodeterminerecoveryefficienciesofoilbydepletionandby gasandwaterdisplacement,shouldenabletheoperatorstomakeamoreprudentselectionof thepressuremaintenanceprogramtobeusedorshoulddemonstratethatapressuremaintenance programwouldnotbesuccessful. Althoughadditionalandreviseddatahavebecomeavailableinsubsequentyears,thefollowingcalculations,whichweremadein1950byreservoirengineers,arebasedondataavailablein1950.Table6.3givesthebasicreservoirdatafortheCanyonReefreservoir.Geologicand otherevidenceindicatedthatthereservoirwasvolumetric(i.e.,thattherewouldbenegligible waterinflux),sothecalculationswerebasedonvolumetricbehavior.Ifanywaterentryshould occur, the effect would be to make the calculations more optimistic—that is, there would be morerecoveryatanyreservoirpressure.Thereservoirwasundersaturated,sotherecoveryfrom Table 6.3 Reservoir Rock and Fluid Properties for the Canyon Reef Reservoir of the Kelly-Snyder Field, Texas (Courtesy The Oil and Gas Journal)14 Initialreservoirpressure 3112psig(at4300ftsubsea) Bubble-pointpressure 1725psig(at4300ftsubsea) Averagereservoirtemperature 125°F Averageporosity 7.7% Averageconnatewater 20% Criticalgassaturation(estimated) 10% Differential liberation analyses of a bottom-hole sample from the Standard Oil Company of Texas at 125°F Pressure (psig) Bo (bbl/STB) Bg (bbl/SCF) Solution GOR (SCF/STB) Bt (bbl/STB) 3112 1.4235 ... 885 1.4235 2800 1.4290 ... 885 1.4290 2400 1.4370 ... 885 1.4370 2000 1.4446 ... 885 1.4446 1725 1.4509 ... 885 1.4509 1700 1.4468 0.00141 876 1.4595 1600 1.4303 0.00151 842 1.4952 1500 1.4139 0.00162 807 1.5403 1400 1.3978 0.00174 772 1.5944 6.4 Kelly-Snyder Field, Canyon Reef Reservoir 173 initialpressuretobubble-pointpressureisbyliquidexpansionandthefractionalrecoveryatthe bubblepointis RF = Bt − Bti 1.4509 − 1.4235 = = 0.0189 or1.89% 1.4509 Bt Basedonaninitialcontentof1.4235reservoirbarrelsor1.00STB,thisisrecoveryof0.0189 STB.Becausethesolutiongasremainsat885SCF/STBdownto1725psig,theproducinggasoilratioandthecumulativeproducedgas-oilratioshouldremainnear885SCF/STBduringthis pressuredecline. Below 1725 psig, a free gas phase develops in the reservoir.As long as this gas phase remainsimmobile,itcanneitherflowtothewellboresnormigrateupwardtodevelopagascap butmustremaindistributedthroughoutthereservoir,increasinginsizeasthepressuredeclines. Becausepressurechangesmuchlessrapidlywithreservoirvoidageforgasesthanforliquids, thereservoirpressuredeclinesatamuchlowerratebelowthebubblepoint.Itwasestimatedthat thegasintheCanyonReefreservoirwouldremainimmobileuntilthegassaturationreacheda valuenear10%oftheporevolume.Whenthefreegasbeginstoflow,thecalculationsbecome quitecomplex(seeChapter10);butaslongasthefreegasisimmobile,calculationsmaybe madeassumingthattheproducinggas-oilratioRatanypressurewillequalthesolutiongas-oil ratioRsoatthepressure,sincetheonlygasthatreachesthewellboreisthatinsolution,thefree gasbeingimmobile.Thentheaverageproducing(daily)gas-oilratiobetweenanytwopressures p1 and p2isapproximately Ravg = Rso1 + Rso 2 2 (6.12) andthecumulativegas-oilratioatanypressureis Rp = ∑ ΔN p × R Np N pb × Rsoi + (N pl − N pb )Ravg1 + (N p 2 − N p1 )Ravg 2 + etc. N pb + (N p1 − N pb ) + (N p 2 − N p1 ) + etc. (6.13) Onthebasisof1.00STBofinitialoil,theproductionatbubble-pointpressureNpbis0.0189STB. Theaverageproducinggas-oilratiobetween1725and1600psigwillbe Ravg1 = 885 + 842 = 864 SCF/STB 2 Chapter 6 174 • Undersaturated Oil Reservoirs Thecumulativerecoveryat1600psigNp1isunknown;however,thecumulativegas-oilratioRpmay beexpressedbyEq.(6.13)as Rp1 = 0.0189 × 885 + ( N p1 − 0.0189 )864 N p1 ThisvalueofRp1maybeplacedinEq.(6.11)togetherwiththePVTvaluesat1600psigas N p1 = 1.4952 − 1.4235 0.0189 × 885 + ( N p1 − 0.0189 )864 1.4952 + 0.00151 − 885 N p1 =0.0486STBat1600psig Inasimilarmanner,therecoveryat1400psigmaybecalculated,theresultsbeingvalidonlyif the gas saturation remains below the critical gas saturation, assumed to be 10% for the present calculations. WhenNpstock-tankbarrelsofoilhavebeenproducedfromavolumetric undersaturated reservoirandtheaveragereservoirpressureisp,thevolumeoftheremainingoilis(N – Np)Bo.Since theinitialporevolumeofthereservoirVp is Vp = NBoi (1 − Swi ) (6.14) andsincetheoilsaturationistheoilvolumedividedbytheporevolume, So = ( N − N p ) Bo (1 − Swi ) ( NBoi ) (6.15) OnthebasisofN=1.00STBinitially,NpisthefractionalrecoveryRF, or Np/N,andEq.(6.15)can bewrittenas B So = (1 − RF )(1 − Swi ) o Boi (6.16) whereSwiistheconnatewater,whichisassumedtoremainconstantforvolumetricreservoirs.Then at1600psig,theoilsaturationis 1.4303 So=(l–0.0486)(l–0.20) 1.4235 6.4 Kelly-Snyder Field, Canyon Reef Reservoir 175 =0.765 Thegassaturationis(1–So – Swi),or Sg=1–0.765–0.200=0.035 Figure 6.4 shows the calculated performance of the Kelly-Snyder Field down to a pressure of 1400 psig. Calculations were not continued beyond this point because the free gas saturation had reached approximately 10%, the estimated critical gas saturation for the reservoir. The graph shows the rapid pressure decline above the bubble point and the predicted flattening below the bubble point.The predictions are in good agreement with the field performance, which is calculated in Table 6.4 using field pressures and production data, and a value of 2.25MMMSTBfortheinitialoilinplace.Theproducinggas-oilratio,column2,increasesinstead ofdecreasing,aspredictedbytheprevioustheory.Thisisduetothemorerapiddepletionofsome portionsofthereservoir—forexample,thosedrilledfirst,thoseoflownetproductivethickness, andthoseinthevicinityofthewellbores.Forthepresentpredictions,itispointedoutthatthe previouscalculationswouldnotbealteredgreatlyifaconstantproducinggas-oilratioof885SCF/ STB(i.e.,theinitialdissolvedratio)hadbeenassumedthroughouttheentirecalculation. Theinitialoilundera40-acreunitoftheCanyonReefreservoirforanetformationthickness of200feetis 3500 Calculated Field data Reservoir pressure, psig 3000 2500 Bubble point 2000 Sg = 3.5% Sg = 10.2 1500 1000 0 2 4 6 8 10 12 Recovery in percent Figure 6.4 Material balance calculations and performance, Canyon Reef reservoir, Kelly-Snyder Field. Chapter 6 176 Table 6.4 • Undersaturated Oil Reservoirs Recovery from Kelly-Snyder Canyon Reef Reservoir Based on Production Data and Measured Average Reservoir Pressures, and Assuming an Initial Oil Content of 2.25 MMM STB (1) (2) (3) (4) (5) Pressure interval (psig) Average producing gas-oil ratio (SCF/ STB) Incremental oil production (MM STB) Cumulative oil production (MM STB) Percentage recovery (N = 2.25 MMM STB) 3312to1771 896 60.421 60.421 2.69 1771to1713 934 11.958 72.379 3.22 1713to1662 971 13.320 85.699 3.81 1662to1570 1023 20.009 105.708 4.70 1570to1561 1045 11.864 117.572 5.23 N= 7758 × 40 × 200 × 0.077 × (1 − 0.20) 1.4235 =2.69MMSTB Then,attheaveragedailywellrateof92BOPDin1950,thetimetoproduce11.35%oftheinitial oil(i.e.,at1400psigwhenthegassaturationiscalculatedtobenear10%)is t= 0.1135 × 2.69 × 10 6 ≅ 9.1 years 92 × 365 Bymeansofthiscalculation,thereservoirengineerswereabletoshowthattherewasnoimmediateneedforacurtailmentofproductionandthattherewasplentyoftimeinwhichtomake furtherreservoirstudiesandcarefullyconsideredplansfortheoptimumpressuremaintenance program.Followingcomprehensiveandexhaustivestudiesbyengineers,thefieldwasunitizedin March1953andplacedunderthemanagementofanoperatingcommittee.Thisgroupproceeded toputintooperationapressuremaintenanceprogramconsistingof(1)waterinjectionintowells locatedalongthelongitudinalaxisofthefieldand(2)shuttinginthehighgas-oilratiowells andtransferringtheirallowablestolowgas-oilratiowells.Thehigh-ratiowellswereshutinas soonasthefieldwasunitized,andwaterinjectionwasstartedin1954.Theoperationhasgone asplanned,andapproximately50%oftheinitialoilinplacehasbeenrecovered,incontrastto approximately25%byprimarydepletion,anincreaseofapproximately600MMSTBofrecoverableoil.15 6.5 6.5 The Gloyd-Mitchell Zone of the Rodessa Field 177 The Gloyd-Mitchell Zone of the Rodessa Field 2300 2100 Average reservoir pressure at 4000-ft subsea 2000 500 1000 Production rate, M STB/day Cumulative production, MM STB Gas–oil ratio 500 80 60 Daily production 0 Current gas–oil ratio, SCF/STB Pressure. psig Manyreservoirsareofthevolumetricundersaturatedtypeandtheirproduction,therefore,iscontrolledlargelybythesolutiongas-drivemechanism.Inmanycases,themechanismisalteredtoa greaterorlesserextentbygravitationalsegregationofthegasandoil,bysmallwaterdrives,and bypressuremaintenance,allofwhichimproverecovery.Theimportantcharacteristicsofthistype ofproductionmaybesummarizedasfollowsandobservedinthegraphofFig.6.5fortheGloydMitchellzoneoftheRodessaField.Abovethebubblepoint,thereservoirisproducedbyliquid expansion,andthereisarapiddeclineinreservoirpressurethataccompaniestherecoveryofa fractionof1%toafewpercentagepointsoftheinitialoilinplace.Thegas-oilratiosremainlow andgenerallynearthevalueoftheinitialsolutiongas-oilratio.Belowthebubblepoint,agasphase developsthat,inmostcases,isimmobileuntilthegassaturationreachesthecriticalgassaturation intherangeofafewpercentagepointsto20%.Duringthisperiod,thereservoirproducesbygas expansion,whichischaracterizedbyamuchslowerdeclineinpressureandgas-oilratiosnearorin somecasesevenbelowtheinitialsolutiongas-oilratio.Afterthecriticalgassaturationisreached, freegasbeginstoflow.Thisreducestheoilflowrateanddepletesthereservoirofitsmainsourceof energy.Bythetimethegassaturationreachesavalueusuallyintherangeof15%to30%,theflow ofoilissmallcomparedwiththegas(highgas-oilratios),andthereservoirgasisrapidlydepleted. 40 20 0 Cumulative production 0 1 2 3 4 Time, years Figure 6.5 Development, production, and reservoir pressure curves for the Gloyd-Mitchell zone, Rodessa Field, Louisiana. Chapter 6 178 • Undersaturated Oil Reservoirs Atabandonment,therecoveriesareusuallyintherangeof10%to25%bythesolutiongas-drive mechanismalone,buttheymaybeimprovedbygravitationalsegregationandthecontrolofhigh gas-oilratiowells. TheproductionoftheGloyd-MitchellzoneoftheRodessaField,Louisiana,isagoodexampleofareservoirthatproducedduringthemajorportionofitslifebythedissolvedgas-drivemechanism.16Reasonablyaccuratedataonthisreservoirrelatingtooilandgasproduction,reservoir pressuredecline,sandthickness,andthenumberofproducingwellsprovideanexcellentexample ofthetheoreticalfeaturesofthedissolvedgas-drivemechanism.TheGloyd-Mitchellzoneispracticallyflatandproducedoilof42.8°APIgravity,which,undertheoriginalbottom-holepressureof 2700psig,hadasolutiongas-oilratioof627SCF/STB.Therewasnofreegasoriginallypresent, andthereisnoevidenceofanactivewaterdrive.Thewellswereproducedathighratesandhada rapiddeclineinproduction.Thebehaviorofthegas-oilratios,reservoirpressures,andoilproductionhadthecharacteristicsexpectedofadissolvedgasdrive,althoughthereissomeevidencethat therewasamodificationoftherecoverymechanisminthelaterstagesofdepletion.Theultimate recoverywasestimatedat20%oftheinitialoilinplace. Manyunsuccessfulattemptsweremadetodecreasethegas-oilratiosbyshuttinginthewells, byblankingoffupperportionsoftheformationinproducingwells,andbyperforatingonlythe lowestsandmembers.Thefailuretoreducethegas-oilratiosistypicalofthedissolvedgas-drive mechanism,becausewhenthecriticalgassaturationisreached,thegas-oilratioisafunctionof thedeclineinreservoirpressureordepletionandisnotmateriallychangedbyproductionrateor completionmethods.Evidentlytherewasnegligiblegravitationalsegregationbywhichanartificial gascapdevelopsandcausesabnormallyhighgas-oilratiosinwellscompletedhighonthestructure orintheupperportionoftheformation. Table6.5givesthenumberofproducingwells,averagedailyproduction,averagegas-oilratio, andaveragepressurefortheGloyd-Mitchellzone.Thedailyoilproductionperwell,monthlyoilproduction,cumulativeoilproduction,monthlygasproduction,cumulativegasproduction,andcumulative gas-oilratioshavebeencalculatedfromthesefigures.Thesourceofdataisofinterest.Thenumberof producingwellsattheendofanyperiodisobtainedeitherfromtheoperatorsinthefield,fromthecompletionrecordsasfiledwiththestateregulatorybody,orfromtheperiodicpotentialtests.Theaverage dailyoilproductionisavailablefromthemonthlyproductionreportsfiledwiththestateregulatorycommission.Accuratevaluesfortheaveragedailygas-oilratioscanbeobtainedonlywhenalltheproduced gasismetered.Alternatively,thisinformationisobtainedfromthepotentialtests.Toobtaintheaverage dailygas-oilratiofrompotentialtestsduringanymonth,thegas-oilratioforeachwellismultipliedby thedailyoilallowableordailyproductionrateforthesamewell,givingthetotaldailygasproduction. Theaveragedailygas-oilratioforanymonthisthetotaldailygasproductionfromallproducingwells dividedbythetotaldailyoilproductionfromallthewellsinvolved.Forexample,ifthegas-oilratioof wellAis1000SCF/STBandthedailyrateis100bbl/dayandtheratioofwellBis4000SCF/STBand thedailyrateis50bbl/day,thentheaveragedailygas-oilratioRofthetwowellsis R= 1000 × 100 + 4000 × 50 = 2000SCF/STB 150 Table 6.5 Average Monthly Production Data, Gloyd-Mitchell Zone of the Rodessa Field (1) (2) (3) (4) (5) (6) (7) (8) (9) (10) (11) Months after start of production Number of wells Average daily oil (barrels) Average daily GOR (SCF/STB) Average pressure (psig) Daily oil per well, (3) ÷ (2) Monthly oil (barrels), 30.4 × (3) Cumulative oil (barrels), Σ(7) Monthly gas (M SCF), (4) × (7) Cumulative gas (M SCF), Σ(9) Cumulative GOR (SCF/STB), 10 ÷ (8) 1 2 400 625 2700a 200 12,160 12,160 7,600 7,600 625 2 1 500 750 500 15,200 27,360 11,400 19,000 694 3 3 700 875 233 21,280 48,640 18,620 37,620 773 4 4 1,300 1,000 325 39,520 88,160 39,520 77,140 875 5 4 1,200 950 300 36,480 124,640 34,656 111,796 897 6 6 1,900 1,000 316 57,760 182,400 57,760 169,556 930 7 12 3,600 1,200 8 16 4,900 1,200 2490 2280 179 9 21 6,100 1,400 10 28 7,500 1,700 11 48 9,800 12 55 11,700 13 59 9,900 2,100 14 65 10,000 15 74 10,200 16 79 11,400 3,200 17 87 10,800 4,100 18 91 9,200 4,800 19 93 9,000 5,300 1250 20 96 8,300 5,900 21 93 7,200 6,800 22 93 6,400 7,500 300 109,440 291,840 131,328 300,884 1031 306 148,960 440,800 178,752 479,636 1088 290 185,440 626,240 259,616 739,252 1181 268 228,000 854,240 387,600 1,127M 1319 1,800 204 297,920 1,152,160 536,256 1,663M 1443 1,900 213 355,680 1,507,840 675,792 2,339M 1551 168 300,960 1,808,800 632,016 2,971M 1643 2,400 154 304,000 2,112,800 729,600 3,701M 1752 2,750 138 310,080 2,422,880 852,720 4,554M 1880 144 346,560 2,769,440 1,108,992 5,662M 2045 124 328,320 3,097,760 1,346,112 7,008M 2262 101 279,680 3,377,440 1,342,464 8,351M 2473 97 273,600 3,651,040 1,450,080 9,801M 2684 1115 86 252,320 3,903,360 1,488,688 11,290M 2892 1000 77 218,880 4,122,240 1,488,384 12,778M 3100 900 69 194,560 4,316,800 1,459,200 14,237M 3298 2070 1860 1650 b (continued) Table 6.5 Average Monthly Production Data, Gloyd-Mitchell Zone of the Rodessa Field (continued) 180 (1) (2) (3) (4) (5) (6) (7) (8) (9) (10) (11) Months after start of production Number of wells Average daily oil (barrels) Average daily GOR (SCF/STB) Average pressure (psig) Daily oil per well, (3) ÷ (2) Monthly oil (barrels), 30.4 × (3) Cumulative oil (barrels), Σ(7) Monthly gas (M SCF), (4) × (7) Cumulative gas (M SCF), Σ(9) Cumulative GOR (SCF/STB), 10 ÷ (8) 23 95 5,800 7,600 825 61 176,320 4,493,120 1,340,032 15,577M 3467 24 94 5,400 7,700 740 57 164,160 4,657,280 1,264,032 16,841M 3616 25 95 5,000 7,800 725 53 152,000 4,809,280 1,185,600 18,027M 3748 26 92 4,400 7,500 565 48 133,760 4,943,040 1,003,200 19,030M 3850 27 94 4,200 7,300 530 45 127,680 5,070,720 932,064 19,962M 3937 28 94 4,000 7,300 500 43 121,600 5,192,320 887,680 20,850M 4016 29 93 3,400 6,800 450 37 103,360 5,295,680 702,848 21,553M 4070 30 95 3,200 6,300 405 34 97,280 5,392,960 612,864 22,165M 4110 31 91 3,100 6,100 350 34 94,240 5,487,200 574,864 22,740M 4144 32 93 2,900 5,700 310 31 88,160 5,575,360 502,512 23,243M 4169 33 92 3,000 5,300 390 33 91,200 5,666,560 483,360 23,726M 4187 34 88 2,900 5,100 300 33 88,160 5,754,720 449,616 24,176M 4201 35 87 2,000 4,900 280 23 60,800 5,815,520 297,920 24,474M 4208 36 90 2,400 4,800 310 27 72,960 5,888,480 350,208 24,824M 4216 37 88 2,100 4,500 300 24 63,840 5,952,320 287,280 25,111M 4219 38 88 2,200 4,500 325 25 66,880 6,019,200 300,960 25,412M 4222 39 87 2,100 4,300 300 24 63,840 6,083,040 274,512 25,687M 4223 40 82 2,000 4,000 275 24 60,800 6,143,840 243,200 25,930M 4220 41 85 2,100 3,600 225 25 63,840 6,207,680 229,824 26,160M 4214 6.5 The Gloyd-Mitchell Zone of the Rodessa Field 181 Thisfigureislowerthanthearithmeticaverageratioof2500SCF/STB.Theaveragegas-oilratio ofalargenumberofwells,then,canbeexpressedby Ravg = ∑ R × qo ∑ qo (6.17) whereR and qoaretheindividualgas-oilratiosandstock-tankoilproductionrates. Figure6.5shows,plottedinblockdiagram,thenumberofproducingwells,thedailygasoilratio,andthedailyoilproductionperwell.Also,inasmoothcurve,pressureisplottedagainst time.Theinitialincreaseindailyoilproductionisduetotheincreaseinthenumberofproducing wellsandnottotheimprovementinindividualwellrates.Ifallthewellshadbeencompletedand putonproductionatthesametime,thedailyproductionratewouldhavebeenaplateau,during thetimeallthewellscouldmaketheirallowables,followedbyanexponentialdecline,whichis shownbeginningat16monthsafterthestartofproduction.Sincethedailyoilallowableanddaily productionofawellaredependentonthebottom-holepressureandgas-oilratio,theoilrecovery islargerforwellscompletedearlyinthelifeofafield.Becausethecontrollingfactorinthistypeof mechanismisgasflowinthereservoir,therateofproductionhasnomaterialeffectontheultimate recovery,unlesssomegravitydrainageoccurs.Likewise,wellspacinghasnoproveneffectonrecovery;however,wellspacingandproductionratedirectlyaffecttheeconomicreturn. Therapidincreaseingas-oilratiosintheRodessaFieldledtotheenactmentofagas-conservationorder.Inthisorder,oilandgasproductionwereallocatedpartlyonavolumetricbasistorestrict productionfromwellswithhighgas-oilratios.Thebasicratioforoilwellswassetat2000SCF/STB. Forleasesonwhichthewellsproducedmorethan2000SCF/STB,theallowableinbarrelsperday perwell,basedonacreageandpressure,wasmultipliedby2000anddividedbythegas-oilratioof thewell.Thiscutinproductionproducedadoublehumpinthedailyproductioncurve. Inadditiontoagraphshowingtheproductionhistoryversustime,itisusuallydesirable tohaveagraphthatshowstheproductionhistoryplottedversusthecumulative produced oil. Figure6.6issuchaplotfortheGloyd-MitchellzonedataandisalsoobtainedfromTable6.5. Thisgraphshowssomefeaturesthatdonotappearinthetimegraph.Forexample,astudyof thereservoirpressurecurveshowstheGloyd-Mitchellzonewasproducingbyliquidexpansion untilapproximately200,000bblwereproduced.Thiswasfollowedbyaperiodofproduction bygasexpansionwithalimitedamountoffreegasflow.Whenapproximately3millionbblhad beenproduced,thegasbegantoflowmuchmorerapidlythantheoil,resultinginarapidincreaseinthegas-oilratio.Inthecourseofthistrend,thegas-oilratiocurvereachedamaximum, thendeclinedasthegaswasdepletedandthereservoirpressureapproachedzero.Thedecline ingas-oilratiobeginningafterapproximately4.5millionbblwereproducedwasduemainlyto theexpansionoftheflowingreservoirgasaspressuredeclined.Thusthesamegas-oilratioin standardcubicfeetperdaygivesapproximatelytwicethereservoirflowrateat400psigasat 800psig;hence,thesurfacegas-oilratiomaydeclineandyettheratiooftherateofflowofgas totherateofflowofoilunder reservoir conditionscontinuestoincrease.Itmayalsobereduced by the occurrence of some gravitational segregation and also, from a quite practical point of 2 1 0 2800 Gas expansion region with some free gas flow Cut back in Bubble production point Decline due to depletion of pressure and decline in well production Pre ssu Accerlerated pressure re decline with rising GOR 13 12 11 10 9 2600 2400 2200 2000 1800 8 1600 7 1400 6 3 Undersaturated Oil Reservoirs Liquid expansion y oil 4 14 Rising daily oil due to development Dail 5 Daily oil × 1000, STB Cumulative GOR, MCF/STB 6 Daily GOR × 1000, SCF/STB 7 • 1200 1000 5 4 800 R e GO ativ mul 3 Cu 2 y Dail 600 GOR 400 200 1 0 Reservoir pressure, psig Chapter 6 182 0 1 2 3 4 5 6 7 0 Cumulative production, MM STB Figure 6.6 History of the Gloyd-Mitchell zone of the Rodessa Field plotted versus cumulative recovery. view,bythefailureofoperatorstomeasureorreportgasproductiononwellsproducingfairly lowvolumesoflow-pressuregas. Theresultsofadifferentialgas-liberationtestonabottom-holesamplefromtheGloydzone showthatthesolutiongas-oilratiowas624SCF/STB,whichisinexcellentagreementwiththeinitial producinggas-oilratioof625SCF/STB.17Intheabsenceofgas-liberationtestsonabottom-hole sample,theinitialgas-oilratioofaproperlycompletedwellineitheradissolvedgasdrive,gascap drive,orwater-drivereservoirisusuallyareliablevaluetousefortheinitialsolutiongas-oilratioof thereservoir.AscanbeseeninFig.6.6,theextrapolationsofthepressure,oilrate,andproducing gas-oilratiocurvesonthecumulativeoilplotallindicateanultimaterecoveryofabout7millionbbl. However,nosuchextrapolationcanbemadeonthetimeplot(seeFig.6.5).Itisalsoofinterestthat, whereasthedailyproducingrateisexponentialonthetimeplot,itisclosetoastraightlineonthe cumulativeoilplot. Theaveragegas-oilratioduringanyproductionintervalandthecumulativegas-oilratiomay beindicatedbyintegralsandshadedareasonatypicaldailygas-oilratioversuscumulativestocktankoilproductioncurve,asshowninFig.6.7.IfRrepresentsthedailygas-oilratioatanytime, and Npthecumulativestock-tankproductionatthesametime,thentheproductionduringashort 6.5 The Gloyd-Mitchell Zone of the Rodessa Field 183 Daily GOR R NP1 dNP NP2 Cumulative STB produced Figure 6.7 Typical daily gas-oil ratio curve for a dissolved gas drive reservoir. intervaloftimeisdNpandthetotalvolumeofgasproducedduringthatproductionintervalisR dNp. Thegasproducedoveralongerperiodwhenthegas-oilratioischangingisgivenby ΔG p = N p2 ∫N p1 R dN p (6.18) TheshadedareabetweenNpl and Np2isproportionaltothegasproducedduringtheinterval.The averagedailygas-oilratioduringtheproductionintervalequalstheareaunderthegas-oilratio curvebetweenNpl and Np2inunitsgivenbythecoordinatescales,dividedbytheoilproducedin theinterval(Np2 – Np1),and N p2 Ravg = ∫N p1 R dN p (6.19) (N p 2 − N p1 ) Thecumulativegas-oilratio,Rp,isthetotalnetgasproduceduptoanyperioddividedbythetotal oilproduceduptothatperiod,or N p2 Rp ∫ = 0 R dN p Np (6.20) Chapter 6 184 • Undersaturated Oil Reservoirs Thecumulativeproducedgas-oilratiowascalculatedinthismannerincolumn11ofTable6.5. Forexample,attheendofthethirdperiod, Rp = 625 × 12, 160 + 750 × 15, 200 + 875 × 21, 280 = 773 SCF/STB 12, 160 + 15, 200 + 21, 280 6.6 Calculations, Including Formation and Water Compressibilities InChapter2,itwasshownthatbothformationandwatercompressibilitiesarefunctionsofpressure.Thissuggeststhatthereareinfactnovolumetricreservoirs—thatis,thoseinwhichthehydrocarbonporevolumeofthereservoirremainsconstant.Hallshowedthemagnitudeoftheeffectof formationcompressibilityonvolumetricreservoircalculations.18Thetermvolumetric,however,is retainedtoindicatethosereservoirsinwhichthereisnowaterinfluxbutinwhichvolumeschange slightlywithpressure,duetotheeffectsjustmentioned. TheeffectofcompressibilitiesabovethebubblepointoncalculationsforNareexamined first.Equation(3.8),withRp = Rsoiabovethebubblepoint,becomes cw Swi + c f N ( Bt − Bti ) + N Bti 1 − Swi Δp + We = N p Bt + BwW p (6.21) ThisequationmayberearrangedtosolveforN: N= N p Bt − We + BwW p cw Swi + c f Bt − Bti + Bti 1 − Swi Δp (6.22) Althoughthisequationisentirelysatisfactory,oftenanoilcompressibility,co,isintroducedwith thefollowingdefiningrelationship: co = Vo − Voi B − Boi = o Voi ( pi − p ) Boi Δp and Bo = Boi + Boico Δp (6.23) Thedefinitionofcousesthesingle-phaseformationvolumefactor,butitshouldbeapparentthat aslongasthecalculationsarebeingconductedabovethebubblepoint,Bo = Bt.IfEq.(6.23)is substitutedintothefirstterminEq.(6.21),theresultis 6.6 Calculations, Including Formation and Water Compressibilities cw Swi + c f Δp = NpBt – We + BwWp N(Bti – Bti)+NBtico Δp + N Bti 1 − Swi 185 (6.24) MultiplyingboththenumeratorandthedenominatorofthetermcontainingcobySoandrealizing thatabovethebubblepointthereisnogassaturation,So=1–Swi,Eq.(6.24)becomes NBti co So Δp + N Bti cw Swi + c f 1− S 1− S wi wi = NpBt – We + BwWp Δp or co So + cw Swi + c f NBti 1 − Swi Δ p = NpBt – We + BwWp (6.25) TheexpressioninbracketsofEq.(6.25)iscalledtheeffective fluid compressibility, ce,whichincludesthecompressibilitiesoftheoil,theconnatewater,andtheformation,or ce = co So + cw Swi + c f 1 − Swi (6.26) Finally,Eq.(6.25)maybewrittenas NBticeΔ p = NpBt – We + BwWp (6.27) Forvolumetricreservoirs,We=0andWpisgenerallynegligible,andEq.(6.27)canberearranged tosolveforN: N= N p Bt ce Δp Bti (6.28) Finally,iftheformationandwatercompressibilities,cf and cw,bothequalzero,thenceissimplyco andEq.(6.28)reducestoEq.(6.8),derivedinsection6.3forproductionabovethebubblepoint. Np N = Bt − Bti Bt Example6.3showstheuseofEqs.(6.22)and(6.28)tofindtheinitialoilinplacefromthepressure-productiondataofareservoirthatallgeologicevidenceindicatesisvolumetric(i.e.,itis boundedonallsidesbyimpermeablerocks).Becausetheequationsarebasicallyidentical,they Chapter 6 186 • Undersaturated Oil Reservoirs givethesamecalculationofinitialoil,51.73MMSTB.Acalculationisalsoincludedtoshow thatanerrorof61%isintroducedbyneglectingtheformationandwatercompressibilities. Example 6.2 Calculating Initial Oil in Place in a Volumetric, Undersaturated Reservoir Given Bti=1.35469bbl/STB Btat3600psig=1.37500bbl/STB Connatewater=0.20 cw=3.6(10)–6 psi–1 Bwat3600psig=1.04bbl/STB cf=5.0(10)–6 psi–1 pi=5000psig Np=1.25MMSTB Δp at3600psig=1400psi Wp=32,000STB We=0 Solution SubstitutingintoEq.(6.22) N= 1, 250, 000(1.37500 ) + 32, 000(1.04 ) 3.6(10 −6 )(0.20 ) + 5.0(10 −6 ) 1.37500 − 1.35469 + 1.35469 (1400 ) 1 − 0.20 =51.73MMSTB theaveragecompressibilityofthereservoiroilis co = Bo − Boi 1.375 − 1.35469 = = 10.71 (10 )−6 psi−1 Boi Δp 1.35469(5000 − 3600 ) andtheeffectivefluidcompressibilitybyEq.(6.26)is ce = [ 0.8(10.71) + 0.2( 3.6 ) + 5.0 ]10 −6 = 17.86 (10 )−66 psi−1 0.8 ThentheinitialoilinplacebyEq.(6.28)withtheWptermfromEq.(6.27)includedis 6.6 Calculations, Including Formation and Water Compressibilities N= 187 1,250,000(1.37500)+32,000(1.04) = 51.73 MM STB 17.86(10)−6 (1400)1.35469 Ifthewaterandformationcompressibilitiesareneglected,ce = co,andtheinitialoilinplaceis calculatedtobe N= 1,250,000(1.37500)+32,000(1.04) = 86.25 MM STB 17.71(10)−6 (1400)1.35469 Ascanbeseenfromtheexamplecalculations,theinclusionofthecompressibilitytermssignificantlyaffectsthevalueofN.Thisistrueabovethebubblepointwheretheoil-producingmechanismisdepletion,ortheswellingofreservoirfluids.Afterthebubblepointisreached,thewater androckcompressibilitieshaveamuchsmallereffectonthecalculationsbecausethegascompressibilityissomuchgreater. WhenEq.(3.8)isrearrangedandsolvedforN,wegetthefollowing: N= N p [ Bt + ( Rp − Rsoi ) Bg ] − We + BwW p cw Swi + c f Bt − Bti + Bti Δp 1 − Swi (6.29) Thisisthegeneralmaterialbalanceequationwrittenforanundersaturatedreservoirbelowthebubblepoint.Theeffectsofwaterandformationcompressibilitiesareaccountedforinthisequation. Example6.3comparesthecalculationsforrecoveryfactor,Np/N,foranundersaturatedreservoir withandwithoutincludingtheeffectsofthewaterandformationcompressibilities. Example 6.3 Calculating Np/N for an Undersaturated Reservoir with No Water Production and Negligible Water Influx Notethecalculationisperformedwithandwithoutincludingtheeffectofcompressibilities.Assume thatthecriticalgassaturationisnotreacheduntilafterthereservoirpressuredropsbelow2200psia. Given pi=4000psia cw=3×10–6 psi–1 pb=2500psia cf=5×10–6 psi–1 Sw=30% φ=10% Chapter 6 188 • Undersaturated Oil Reservoirs Pressure (psia) Rso (SCF/STB) Bg (bbl/SCF) Bt (bbl/SCF) 4000 1000 0.00083 1.3000 2500 1000 0.00133 1.3200 2300 920 0.00144 1.3952 2250 900 0.00148 1.4180 2200 880 0.00151 1.4412 Solution Thecalculationsareperformedfirstbyincludingtheeffectofcompressibilities.Equation(6.22), withWp equaltozeroandWeneglected,isthenrearrangedandusedtocalculatetherecoveryat thebubblepoint. cw Swi + c f Bt − Bti + Bti Δp 1 − Swi = N Bt Np 3(10 −6 )0.3 + 5(10 −6 ) 1.32 − 1.30 + 1.30 1500 Np 1 − 0.3 = = 0.0276 N 1.32 Belowthebubblepoint,Eqs.(6.29)and(6.13)areusedtocalculatetherecovery: cw Swi + c f Bt − Bti + Bti Np 1 − Swi = N Bt + ( R p − Rsoi )B Bg Δp and Rp = ∑ ( ΔN p ) R Np = ∑ ( ΔN p / N ) R Np / N Duringthepressureincrement2500–2300psia,thecalculationsyield 3(10 −6 )0.3 + 5(10 −6 ) 1.3952 − 1.30 + 1.30 1700 Np 1 − 0.3 = 1.3952 + ( Rp − 1000 )0.00144 N 6.6 Calculations, Including Formation and Water Compressibilities 189 0.0276(1000 ) + ( N p / N − 0.0276 ) Rave1 Rp = Np / N whereRave1equalstheaveragevalueofthesolutionGORduringthepressureincrement. Rave1 = 1000 + 920 = 960 2 SolvingthesethreeequationsforNp/N yields Np N = 0.08391 Repeatingthecalculationsforthepressureincrement2250–2200psia,theNp/Nisfoundtobe Np N = 0.11754 Now,thecalculationsareperformedbyassumingthattheeffectofincludingthecompressibilityterms isnegligible.Forthiscase,atthebubblepoint,therecoverycanbecalculatedbyusingEq.(6.8): Np = N Bt − Bti 1.32 − 1.30 = = 0.01515 1.32 Bt Belowthebubblepoint,Eqs.(6.11)and(6.13)areusedtocalculateNp/N Np N = Bt − Bti Bt + ( R p − Rsoi ) Bg and Rp = ∑ ( ΔN p ) R Np = ∑ ( ΔN p / N ) R Np / N Forthepressureincrement2500–2300psia, Np N = 1.3952 − 1.30 1.3952 + ( Rp − 1000 )0.00144 Chapter 6 190 Rp = • Undersaturated Oil Reservoirs 0.01515(1000 ) + ( N p / N − 0.01515 ) Rave1 Np / N whereRave1isgivenby Rave1 = 1000 + 920 = 960 2 Solvingthesethreeequationsyields Np N = 0.07051 Repeatingthecalculationsforthepressureincrement2300–2250psia, Np N = 0.08707 Forthepressureincrement2250–2200psia, Np N = 0.10377 Figure6.8isaplotoftheresultsforthetwodifferentcases—thatis,withandwithoutconsidering thecompressibilityterm. Thecalculationssuggestthereisaverysignificantdifferenceintheresultsofthetwocases, downtothebubblepoint.Thedifferenceistheresultofthefactthattherockandwatercompressibilitiesareonthesameorderofmagnitudeastheoilcompressibility.Byincludingthem,thefractional recovery has been significantly affected. The case that used the rock and water compressibilities comesclosertosimulatingrealproductionabovethebubblepointfromthistypeofreservoir.Thisis becausetheactualmechanismofoilproductionistheexpansionoftheoil,water,androckphases; thereisnofreegasphase. Below the bubble point, the magnitude of the fractional recoveries calculated by the two schemesstilldifferbyaboutwhatthedifferencewasatthebubblepoint,suggestingthatbelowthe bubblepoint,thecompressibilityofthegasphaseissolargethatthewaterandrockcompressibilitiesdonotcontributesignificantlytothecalculatedfractionalrecoveries.Thiscorrespondstothe actualmechanismofoilproductionbelowthebubblepoint,wheregasiscomingoutofsolution andfreegasisexpandingasthereservoirpressuredeclines. TheresultsofthecalculationsofExample6.4aremeanttohelpthereadertounderstandthe fundamentalproductionmechanismsthatoccurinundersaturatedreservoirs.Theyarenotmeant Problems 191 5000 With compressibility terms Without compressibility terms Pressure 4000 3000 2000 0 0.02 0.04 0.06 0.08 0.10 0.12 Fractional recovery Figure 6.8 Pressure versus fractional recovery for the calculations of Problem 6.4 tosuggestthatthecalculationscanbemadeeasierbyignoringtermsinequationsforparticular reservoirsituations.Thecalculationsarerelativelyeasytoperform,whetherornotalltermsare included.Sincenearlyallcalculationsareconductedwiththeuseofacomputer,thereisnoneed toneglecttermsfromtheequations. Problems 6.1 Usingthelettersymbolsforreservoirengineering,writeexpressionsforthefollowingterms foravolumetric,undersaturatedreservoir: (a) (b) (c) (d) (e) (f) (g) (h) Theinitialreservoiroilinplaceinstock-tankbarrels ThefractionalrecoveryafterproducingNp STB Thevolumeoccupiedbytheremainingoil(liquid)afterproducingNp STB TheSCFofgasproduced TheSCFofinitialgas TheSCFofgasinsolutionintheremainingoil Bydifference,theSCFofescapedorfreegasinthereservoirafterproducingNp STB Thevolumeoccupiedbytheescaped,orfree,gas Chapter 6 192 • Undersaturated Oil Reservoirs 6.2 Thephysicalcharacteristicsofthe3–A–2reservoiraregiveninFig.6.2: (a) Calculate the percentage of recovery, assuming this reservoir could be produced at a constantcumulativeproducedgas-oilratioof1100SCF/STB,whenthepressurefallsto 3550,2800,2000,1200,and800psia.Plotthepercentageofrecoveryversuspressure. (b) TodemonstratetheeffectofincreasedGORonrecovery,recalculatetherecoveries, assumingthatthecumulativeproducedGORis3300SCF/STB.Plotthepercentageof recoveryversuspressureonthesamegraphusedforthepreviousproblem. (c) Toafirstapproximation,whatdoestriplingtheproducedGORdotothepercentageof recovery? (d) Doesthismakeitappearreasonablethat,toimproverecovery,high-ratio(GOR)wells shouldbeworkedoverorshutinwhenfeasible? 6.3 If1millionSTBofoilhavebeenproducedfromthe3–A–2reservoiratacumulativeproduced GORof2700SCF/STB,causingthereservoirpressuretodropfromtheinitialreservoirpressureof4400psiato2800psia,whatistheinitialstock-tankoilinplace? 6.4 Thefollowingdataaretakenfromanoilfieldthathadnooriginalgascapandnowater drive: Oilporevolumeofreservoir=75MMft3 Solubilityofgasincrude=0.42SCF/STB/psi Initialbottom-holepressure=3500psia Bottom-holetemperature=140°F Bubble-pointpressureofthereservoir=2400psia Formationvolumefactorat3500psia=1.333bbl/STB Compressibilityfactorofthegasat1500psiaand140°F=0.95 Oilproducedwhenpressureis1500psia=1.0MMSTB NetcumulativeproducedGOR=2800SCF/STB CalculatetheinitialSTBofoilinthereservoir. CalculatetheinitialSCFofgasinthereservoir. CalculatetheinitialdissolvedGORofthereservoir. CalculatetheSCFofgasremaininginthereservoirat1500psia. CalculatetheSCFoffreegasinthereservoirat1500psia. Calculatethegasvolumefactoroftheescapedgasat1500psiaatstandardconditions of14.7psiaand60°F. (g) Calculatethereservoirvolumeofthefreegasat1500psia. (h) CalculatethetotalreservoirGORat1500psia. (i) CalculatethedissolvedGORat1500psia. (j) Calculatetheliquidvolumefactoroftheoilat1500psia. (a) (b) (c) (d) (e) (f) Problems 193 1.28 575 0.87 ef m lu 1.24 n tio vo F 1.22 0.85 R a m or 0.86 tio O nG lu So 0.84 or fact iation v e d s a G 0.83 0.82 0.81 1.20 550 525 500 475 450 425 400 Solution GOR, SCF/STB r to ac 1.26 Gas deviation factor Formation volume factor, bbl/STB 1.30 375 350 1500 Figure 6.9 1600 1700 1800 1900 2000 2100 Pressure, psia 2200 2300 2400 2500 PVT data for the R Sand reservoir at 150°F. (k) Calculatethetotal,ortwo-phase,oilvolumefactoroftheoilanditsinitialcomplement ofdissolvedgasat1500psia. 6.5 (a) C ontinuingthecalculationsoftheKelly-SnyderField,calculatethefractionalrecovery andthegassaturationat1400psig. (b) Whatisthedeviationfactorforthegasat1600psigand125°F? 6.6 TheRSandisavolumetricoilreservoirwhosePVTpropertiesareshowninFig.6.9.When thereservoirpressuredroppedfromaninitialpressureof2500psiatoanaveragepressureof 1600psia,atotalof26.0MMSTBofoilwasproduced.ThecumulativeGORat1600psia is954SCF/STB,andthecurrentGORis2250SCF/STB.Theaverageporosityforthefield is18%,andaverageconnatewateris18%.Noappreciableamountofwaterwasproduced, andstandardconditionswere14.7psiaand60°F. Calculatetheinitialoilinplace. CalculatetheSCFofevolvedgasremaininginthereservoirat1600psia. Calculatetheaveragegassaturationinthereservoirat1600psia. Calculatethebarrelsofoilthatwouldhavebeenrecoveredat1600psiaifalltheproducedgashadbeenreturnedtothereservoir. (e) Calculatethetwo-phasevolumefactorat1600psia. (f) Assumingnofreegasflow,calculatetherecoveryexpectedbydepletiondriveperformancedownto2000psia. (g) CalculatetheinitialSCFoffreegasinthereservoirat2500psia. (a) (b) (c) (d) Chapter 6 194 • Undersaturated Oil Reservoirs 6.7 IfthereservoirofProblem6.6hadbeenawater-drivereservoir,inwhich25×106bblof waterhadencroachedintothereservoirwhenthepressurehadfallento1600psia,calculate theinitialoilinplace.UsethesamecurrentandcumulativeGORs,thesamePVTdata,and assumenowaterproduction. 6.8 Thefollowingproductionandgasinjectiondatapertaintoareservoir. Cumulative oil production, Np (MM STB) Average daily gas-oil ratio, R (SCF/STB) Cumulative gas injected, GI (MM SCF) 0 300 0 1 280 0 2 280 0 3 340 0 4 560 0 5 850 0 6 1120 520 7 1420 930 8 1640 1440 9 1700 2104 10 1640 2743 (a) CalculatetheaverageproducingGORduringtheproductionintervalfrom6MMSTB to8MMSTB. (b) WhatisthecumulativeproducedGORwhen8MMSTBhasbeenproduced? (c) CalculatethenetaverageproducingGORduringtheproductionintervalfrom6MM STBto8MMSTB. (d) WhatisthenetcumulativeproducedGORwhen8MMSTBhasbeenproduced? (e) PlotonthesamegraphtheaveragedailyGOR,thecumulativeproducedgas,thenetcumulativeproducedgas,andthecumulativeinjectedgasversuscumulativeoilproduction. 6.9 An undersaturated reservoir producing above the bubble point had an initial pressure of 5000psia,atwhichpressuretheoilvolumefactorwas1.510bbl/STB.Whenthepressure droppedto4600psia,owingtotheproductionof100,000STBofoil,theoilvolumefactor was1.520bbl/STB.Theconnatewatersaturationwas25%,watercompressibility3.2×10–6 psi–1,andbasedonanaverageporosityof16%,therockcompressibilitywas4.0×10–6 psi–1. Theaveragecompressibilityoftheoilbetween5000and4600psiarelativetothevolumeat 5000psiawas17.00×10–6 psi–1. (a) Geologicevidenceandtheabsenceofwaterproductionindicatedavolumetricreservoir.Assumingthiswasso,whatwasthecalculatedinitialoilinplace? Problems 195 (b) Itwasdesiredtoinventorytheinitialstock-tankbarrelsinplaceatasecondproductioninterval.Whenthepressurehaddroppedto4200psia,formationvolumefactor 1.531bbl/STB,205MSTBhadbeenproduced.Iftheaverageoilcompressibilitywas 17.65×10–6 psi–1,whatwastheinitialoilinplace? (c) Whenallcoresandlogshadbeenanalyzed,thevolumetricestimateoftheinitialoilin placewas7.5MMSTB.Ifthisfigureiscorrect,howmuchwaterenteredthereservoir whenthepressuredeclinedto4600psia? 6.10 Estimatethefractionrecoveryfromasandstonereservoirbywaterdriveifthepermeability is1500md,theconnatewateris20%,thereservoiroilviscosityis1.5cp,theporosityis 25%,andtheaverageformationthicknessis50ft. 6.11 ThefollowingPVTdataareavailableforareservoir,whichfromvolumetricreserveestimationisconsideredtohave275MMSTBofoilinitiallyinplace.Theoriginalpressurewas 3600psia.Thecurrentpressureis3400psia,and732,800STBhavebeenproduced.How muchoilwillhavebeenproducedbythetimethereservoirpressureis2700psia? Pressure (psia) Solution gas oil ratio (SCF/STB) Formation volume factor (bbl/STB) 3600 567 1.310 3200 567 1.317 2800 567 1.325 2500 567 1.333 2400 554 1.310 1800 434 1.263 1200 337 1.210 600 223 1.140 200 143 1.070 6.12 Productiondata,alongwithreservoirandfluiddata,foranundersaturatedreservoirfollow. Therewasnomeasurablewaterproduced,anditcanbeassumedthattherewasnofreegas flowinthereservoir.Determinethefollowing: (a) Saturationsofoil,gas,andwateratareservoirpressureof2258. (b) Haswaterencroachmentoccurredand,ifso,whatisthevolume? Gasspecificgravity=0.78 Reservoirtemperature=160°F Initialwatersaturation=25% Originaloilinplace=180MMSTB Bubble-pointpressure=2819psia Chapter 6 196 • Undersaturated Oil Reservoirs ThefollowingexpressionsforBo and Rso,asfunctionsofpressure,weredetermined fromlaboratorydata: Bo=1.00+0.00015p(inbbl/STB) Rso=50+0.42p(inSCF/STB) Pressure (psia) Cumulative oil produced (STB) Cumulative gas produced (SCF) Instantaneous GOR (SCF/STB) 2819 0 0 1000 2742 4.38MM 4.38MM 1280 2639 10.16MM 10.36MM 1480 2506 20.09MM 21.295MM 2000 2403 21.02MM 30.26MM 2500 2258 34.29MM 41.15MM 3300 6.13 The following table provides fluid property data for an initially undersaturated lens type of oil reservoir.The initial connate water saturation was 25%. Initial reservoir temperature and pressure were 97°F and 2110 psia, respectively. The bubble-point pressurewas1700psia.Averagecompressibilityfactorsbetweentheinitialandbubble-point pressures were 4.0 × 10–6 psi–1 and 3.1 × 10–6 psi–1 for the formation and water,respectively.Theinitialoilformationvolumefactorwas1.256bbl/STB.The criticalgassaturationisestimatedtobe10%.Determinetherecoveryversuspressure curveforthisreservoir. Pressure (psia) Oil formation volume factor (bbl/STB) Solution GOR (SCF/STB) Gas formation volume factor (ft3/SCF) 1700 1.265 540 0.007412 1500 1.241 490 0.008423 1300 1.214 440 0.009826 1100 1.191 387 0.011792 900 1.161 334 0.014711 700 1.147 278 0.019316 500 1.117 220 0.027794 6.14 The Wildcat reservoir was discovered in 1970. The reservoir had an initial pressure of3000psia,andlaboratorydataindicatedabubble-pointpressureof2500psia.The connatewatersaturationwas22%.Calculatethefractionalrecovery,Np/N,frominitial References 197 conditionsdowntoapressureof2300psia.Stateanyassumptionsyoumakerelativeto thecalculations. Porosity=0.165 Formationcompressibility=2.5×10–6 psi–1 Reservoirtemperature=150°F Pressure (psia) Bo (bbl/STB) Rso (SCF/S TB) z Bg (bbl/SCF) Viscosity ratio (μo/μg) 3000 1.315 650 0.745 0.000726 53.91 2500 1.325 650 0.680 0.000796 56.60 2300 1.311 618 0.663 0.000843 61.46 References 1. T. L. Kennerly, “Oil Reservoir Fluids (Sampling,Analysis, andApplication of Data),” presentedbeforetheDeltaSectionofAlME,Jan.1953(availablefromCoreLaboratories,Inc., Dallas). 2. FrankO.Reudelhuber,“SamplingProceduresforOilReservoirFluids,”Jour. of Petroleum Technology(Dec.1957),9,15–18. 3. RalphH.EspachandJosephFry,“VariableCharacteristicsoftheOilintheTensleepSandstoneReservoir,ElkBasinField,WyomingandMontana,”Trans.AlME(1951),192,75. 4. CecilQ.Cupps,PhilipH.LipstateJr.,andJosephFry,“VarianceinCharacteristicsintheOil in theWeber Sandstone Reservoir, Rangely Field, Colo.,” US Bureau of Mines R.I. 4761, U.S.D.I.,Apr.1951;seealsoWorld Oil(Dec.1957),133,No.7,192. 5. A.B.Cook,G.B.Spencer,F.P.Bobrowski,andTimChin,“ANewMethodofDeterminingVariationsinPhysicalPropertiesofOilinaReservoir,withApplicationtotheScurry Reef Field, Scurry County, Tex,” US Bureau of Mines R.I. 5106, U.S.D.I., Feb. 1955, 12–23. 6. D.R.McCord,“PerformancePredictionsIncorporatingGravityDrainageandGasCapPressureMaintenance—LL-370Area,BolivarCoastalField,”Trans.AlME(1953),198,232. 7. J.J.Arps,“EstimationofPrimaryOilReserves,”Trans.AlME(1956),207,183–86. 8. R.C.CrazeandS.E.Buckley,“AFactualAnalysisoftheEffectofWellSpacingonOilRecovery,”API Drilling and Production Practice(1945),144–55. 9. J.J.ArpsandT.G.Roberts,“TheEffectofRelativePermeabilityRatio,theOilGravity,and theSolutionGas-OilRatioonthePrimaryRecoveryfromaDepletionTypeReservoir,”Trans. AlME(1955),204,120–26. 198 Chapter 6 • Undersaturated Oil Reservoirs 10. H. G. Botset and M. Muskat, “Effect of Pressure Reduction upon Core Saturation,” Trans. AlME(1939),132,172–83. 11. R. K. Guthrie and Martin K. Greenberger, “The Use of Multiple CorrelationAnalyses for Interpreting Petroleum-Engineering Data,” API Drilling and Production Practice (1955), 135–37. 12. StewartE.Buckley,Petroleum Conservation,AmericanInstituteofMiningandMetallurgical Engineers,1951,239. 13. K.B.BarnesandR.F.Carlson,“ScurryAnalysis,”Oil and Gas Jour.(1950),48,No.51,64. 14. “Material-Balance Calculations, North Snyder Field Canyon Reef Reservoir,” Oil and Gas Jour.(1950),49,No.1,85. 15. R.M.Dicharry,T.L.Perryman,andJ.D.Ronquille,“EvaluationandDesignofaCO2MiscibleFloodProject—SACROCUnit,Kelly-SnyderField,”Jour. of Petroleum Technology, Nov. 1973,1309–18. 16. Petroleum Reservoir Efficiency and Well Spacing, Standard Oil Development Company, 1943,22. 17. H.B.HillandR.K.Guthrie,“EngineeringStudyoftheRodessaOilFieldinLouisiana,Texas, andArkansas,”USBureauofMinesR.I.3715,1943,87. 18. HowardN.Hall,“CompressibilityofReservoirRocks,”Trans.AlME(1953),198,309. C H A P T E R 7 Saturated Oil Reservoirs 7.1 Introduction Thefinalreservoirtypeisthesaturatedoilreservoirandisdistinguishedbythepresenceofbothliquid andgasinthereservoir.ThematerialbalanceequationsdiscussedinChapter6,forundersaturatedoil reservoirs,applytovolumetricandwater-drivereservoirsinwhichtherearenoinitialgascaps.However, theequationsapplytoreservoirsinwhichanartificialgas-capforms,owingeithertogravitationalsegregationoftheoilandfreegasphasesbelowthebubblepointortotheinjectionofgas,usuallyinthehigher structuralportionsofthereservoir.Whenthereisaninitialgascap(i.e.,theoilisinitiallysaturated),there isnegligibleliquidexpansionenergy.However,theenergystoredinthedissolvedgasissupplementedby thatinthecap,anditisnotsurprisingthatrecoveriesfromgas-capreservoirsaregenerallyhigherthan fromthosewithoutcaps,otherthingsremainingequal.Thischapterwillbeginwithareviewofthefactors thataffecttheoverallrecoveryofsaturatedoilreservoirsandtheapplicationofthematerialbalanceused throughoutthetext.Driveindices,introducedinChapter3,arerevisited,astheyaremostapplicableto thesetypesofreservoirsandquantitativelydemonstratetheproportionaleffectofagivenmechanism ontheproduction.TheHavlena-Odehmethodwillbeappliedtoprovideatoolforearlypredictionof reservoirbehavior,followedbytoolstounderstandandpredictgas-liquidseparation.Thechapterwill concludewithadiscussionofvolatilereservoirsandtheconceptofamaximumefficientrate(MER). 7.1.1 Factors Affecting Overall Recovery Ingas-capdrives,asproductionproceedsandreservoirpressuredeclines,theexpansionofthegasdisplacesoildownwardtowardthewells.Thisphenomenonisobservedintheincreaseofthegas-oilratios insuccessivelylowerwells.Atthesametime,byvirtueofitsexpansion,thegascapretardspressure declineandthereforetheliberationofsolutiongaswithintheoilzone,thusimprovingrecoveryby reducingtheproducinggas-oilratiosofthewells.Thismechanismismosteffectiveinthosereservoirs ofmarkedstructuralrelief,whichintroducesaverticalcomponentoffluidflow,wherebygravitational segregationoftheoilandfreegasinthesandmayoccur.1Therecoveriesfromvolumetricgas-capreservoirswilltypicallybehigherthantherecoveriesforundersaturatedreservoirsandwillbeevenhigher forlargegascaps,continuousuniformformations,andgoodgravitationalsegregationcharacteristics. 199 Chapter 7 200 • Saturated Oil Reservoirs 7.1.1.1 Large Gas Caps Thesizeofthegascapisusuallyexpressedrelativetothesizeoftheoilzonebytheratiom, as definedinChapter3. 7.1.1.2 Continuous Uniform Formations Continuousuniformformationsreducethechannelingoftheexpandinggascapaheadoftheoil andthebypassingofoilinthelesspermeableportions. 7.1.1.3 Good Gravitational Segregation Characteristics These characteristics include primarily (1) pronounced structure, (2) low oil viscosity, (3) high permeability,and(4)lowoilvelocities. Water drive and hydraulic controlaretermsusedindesignatingamechanismthatinvolvesthemovementofwaterintothereservoirasgasandoilareproduced.Waterinfluxintoareservoirmaybeedgewaterorbottomwater,thelatterindicatingthattheoilisunderlainbyawaterzoneofsufficientthickness sothatthewatermovementisessentiallyvertical.Themostcommonsourceofwaterdriveisaresult ofexpansionofthewaterandthecompressibilityoftherockintheaquifer;however,itmayresultfrom artesianflow.Theimportantcharacteristicsofawater-driverecoveryprocessarethefollowing: 1. Thevolumeofthereservoirisconstantlyreducedbythewaterinflux.Thisinfluxisasource ofenergyinadditiontotheenergyofliquidexpansionabovethebubblepointandtheenergy storedinthesolutiongasandinthefree,orcap,gas. 2. Thebottom-holepressureisrelatedtotheratioofwaterinfluxtovoidage.Whenthevoidage onlyslightlyexceedstheinflux,thereisonlyaslightpressuredecline.Whenthevoidage considerablyexceedstheinflux,thepressuredeclineispronouncedandapproachesthatfor gas-capordissolvedgas-drivereservoirs,asthecasemaybe. 3. Foredgewaterdrives,regionalmigrationispronouncedinthedirectionofthehigherstructuralareas. 4. Asthewaterencroachesinbothedgewaterandbottomwaterdrives,thereisanincreasing volumeofwaterproduced,andeventuallywaterisproducedbyallwells. 5. Underfavorableconditions,theoilrecoveriescanbequitehigh. 7.2 Material Balance in Saturated Reservoirs ThegeneralSchilthuismaterialbalanceequationwasdevelopedinChapter3andisasfollows: N(Bt – Bti)+ cw Swi + c f NmBti (Bg –Bgi)+(1+m)NBti Bgi 1 − Swi = Np[Bt + (Rp – Rsoi)Bg] + BwWp Δp + We (3.7) 7.2 Material Balance in Saturated Reservoirs 201 Equation(3.7)canberearrangedandsolvedforN,theinitialoilinplace: N= N p [ Bt + ( Rp − Rsoi ) Bg ] − We + BwW p cw Swi + c f mBti Bt − Bti + ( Bg − Bgi ) + (1 + m ) Bti Bgi 1 − Swi Δp (7.1) Iftheexpansiontermduetothecompressibilitiesoftheformationandconnatewatercanbeneglected,astheyusuallyareinasaturatedreservoir,thenEq.(7.1)becomes N= N p [ Bt + ( Rp − Rsoi ) Bg ] − We + BwW p mBti Bt − Bti + ( Bg − Bgi ) Bgi (7.2) Example7.1showstheapplicationofEq.(7.2)tothecalculationofinitialoilinplaceforawaterdrivereservoirwithaninitialgascap.Thecalculationsaredoneoncebyconvertingallbarrelunits tocubicfeetunitsandthenasecondtimebyconvertingallcubicfeetunitstobarrelunits.Itdoes notmatterwhichsetofunitsisused,onlythateachtermintheequationisconsistent.Problems sometimesarisebecausegasformationvolumefactorsarereportedeitherinft3/SCForinbbl/SCF. Typically,whenapplyingthematerialbalanceequationforaliquidreservoir,gasformationvolume factorsarereportedinbbl/SCF.Usecaretoensurethattheunitsarecorrect. Example 7.1 Calculating the Stock-Tank Barrels of Oil Initially-in-Place in a Combination Drive Reservoir Given Volumeofbulkoilzone=112,000ac-ft Volumeofbulkgaszone=19,600ac-ft Initialreservoirpressure=2710psia Initialformationvolumefactor=1.340bbl/STB Initialgasvolumefactor=0.006266ft3/SCF InitialdissolvedGOR=562SCF/STB Oilproducedduringtheinterval=20MMSTB Reservoirpressureattheendoftheinterval=2000psia AverageproducedGOR=700SCF/STB Two-phaseformationvolumefactorat2000psia=1.4954bbl/STB Volumeofwaterencroached=11.58MMbbl Volumeofwaterproduced=1.05MMSTB Formationvolumefactorofthewater=1.028bbl/STB Gasvolumefactorat2000psia=0.008479ft3/SCF Chapter 7 202 • Saturated Oil Reservoirs Solution IntheuseofEq.(7.2), Bti=1.3400×5.615=7.5241ft3/STB Bt=1.4954×5.615=8.3967ft3/STB We=11.58×5.615=65.02MMft3 Bw =1.028×5.615 = 5.772 ft3/STB BwWp=1.028×5.615x1.05=6.06MMresft3 Assumingthesameporosityandconnatewaterfortheoilandgaszones, m= GBgi NBoi = Volume of bulk oil 19,600 = = 0.175 Volume of bulk gas 112,000 SubstitutinginEq.(7.2)withallbarrelunitsconvertedtocubicfeetunits, N= N= N p [ Bt + ( Rp − Rsoi ) Bg ] − We + BwW p mBti Bt − Bti + ( Bg − Bgi ) Bgi (7.2) 20 × 10 6 [ 8.3967 + ( 700 − 562 )0.008479 ] − 65.02 + 6.06 × 10 6 7.5241 (0.008479 − 0.006266 ) 8.3967 − 7.5241 + 0.175 0.0006266 =99.0MMSTB ThecalculationwillberepeatedusingEq.(7.2),withBtinbarrelsperstock-tankbarrel,Bg in barrelsperstandardcubicfoot,andWe and Wpinbarrels. N= 7.2.1 20 × 10 6 [1.4954 + ( 700 − 562 )0.001510 ] − 11.588 + 1.05 × 1.028 × 10 6 1.3400 1.4954 − 1.3400 + 0.175 + (0.001510 − 0.001116 ) 0.001116 =99.0MMSTB The Use of Drive Indices in Material Balance Calculations InChapter3,theconceptofdriveindices,firstintroducedtothereservoirengineeringliteratureby Pirson,wasdeveloped.2Toillustratetheuseofthesedriveindices,calculationsareperformedonthe ConroeField,Texas.Figure7.1showsthepressureandproductionhistoryoftheConroeField,and 7.2 Material Balance in Saturated Reservoirs 203 2300 2100 Average reservoir pressure at 4000-ft subsea 2000 500 1000 Production rate, M STB/day Cumulative production, MM STB Gas–oil ratio 500 80 60 0 Daily production Current gas–oil ratio, SCF/STB Pressure. psig Fig.7.2givesthegasandtwo-phaseoilformationvolumefactorforthereservoirfluids.Table7.1 containsotherreservoirandproductiondataandsummarizesthecalculationsincolumnformfor threedifferentperiods. 40 20 0 Cumulative production 0 1 2 3 4 Time, years Figure 7.1 Reservoir pressure and production data, the Conroe Field (after Schilthuis, trans. AlME).3 Two-phase oil volume factor, ft3 per STB 7.4 8.2 9.0 9.8 10.6 2200 Pressure, psig 2000 1800 1600 1400 1200 0.006 0.008 0.010 0.012 0.014 Gas volume factor, ft3 per SCF Figure 7.2 Pressure volume relations for the Conroe Field oil and original complement of dissolved gas (after Schilthuis, trans. AlME).3 Chapter 7 204 • Saturated Oil Reservoirs Table 7.1 Material Balance Calculation of Water Influx or Oil in Place for Oil Reservoirs below the Bubble-Point Pressure For the Conroe Field, Bti=7.37ft3/STB Bgi=0.00637ft3/SCF(14.4psiaand60°F) 181, 225 ac-ft m= = 0.224 810, 000 ac-ft mBti/Bgi=259SCF/STB Rsoi=600SCF/STB Line number Quantity Units 12 18 24 30 36 1 Np MMSTB 9.070 22.34 32.03 40.18 48.24 2 Rp SCF/STB 1630 1180 1070 1025 995 3 p psig 2143 2108 2098 2087 2091 Bg ft /SCF 0.00676 0.00687 0.00691 0.00694 0.00693 5 Bt ft /STB 7.46 7.51 7.51 7.53 7.52 6 NpRp MMSCF 14,800 34,400 48,100 7 Rp– Rsoi SCF/STB 1030 470 395 8 (Rp– Rsoi) Bg ft /STB 6.95 3.24 2.74 9 (5)+(8) ft3/STB 14.41 10.75 10.26 10 Bg– Bgi ft /SCF 0.00039 0.00054 0.00056 11 (10)× (mBti/Bgi) ft /STB 0.101 0.137 0.145 12 Bt– Bti ft3/STB 0.09 0.14 0.15 13 (11)+ (12) ft3/STB 0.191 0.277 0.295 14 (1)×(9) MMft3 131 345 495 15 We– Wp 3 MMft 51.5 178 320 16 (14)–(15) MMft3 79.5 167 175 17 N =(16)/ (13) MMSTB 415 602 594 18 DDI Fraction 0.285 0.244 0.180 19 SDI Fraction 0.320 0.239 0.174 20 WDI Fraction 0.395 0.516 0.646 4 3 3 3 3 3 Months after start of production 7.2 Material Balance in Saturated Reservoirs 205 The use of such tabular forms is common in many calculations of reservoir engineering in theinterestofstandardizingandsummarizingcalculationsthatmaynotbereviewedorrepeatedfor intervalsofmonthsorsometimeslonger.Theuseofspreadsheetsmakesthesecalculationsmuch easierandmaintainsthetabularform.Theyalsoenableanengineertotakeovertheworkofapredecessorwithaminimumofbriefingandstudy.Tabularformsalsohavetheadvantageofprovidingata glancethecomponentpartsofacalculation,manyofwhichhavesignificancethemselves.Themore importantfactorscanbereadilydistinguishedfromthelessimportantones,andtrendsinsomeofthe componentpartsoftenprovideinsightintothereservoirbehavior.Forexample,thevaluesofline11 inTable7.1showtheexpansionofthegascapoftheConroeFieldasthepressuredeclines.Line17 showsthevaluesoftheinitialoilinplacecalculatedatthreeproductionintervals.Thesevaluesand otherscalculatedelsewhereareplottedversuscumulativeproductioninFig.7.3,whichalsoincludes therecoveryateachperiod,expressedasthepercentageofcumulativeoilintheinitialoilinplace, ascalculatedatthatperiod.Theincreasingvaluesoftheinitialoilduringtheearlylifeofthefield maybeexplainedbysomeofthelimitationsofthematerialbalanceequationdiscussedinChapter3, particularlytheaveragereservoirpressure.Lowervaluesoftheaveragereservoirpressureinthemore permeableandinthedevelopedportionofthereservoircausethecalculatedvaluesoftheinitialoil tobelow,throughtheeffectontheoilandgasvolumefactors.TheindicationsofFig.7.3arethatthe reservoircontainsapproximately600MMSTBofinitialoilandthatreliablevaluesoftheinitialoil arenotobtaineduntilabout5%oftheoilhasbeenproduced.Thisisnotauniversalfigurebutdepends onanumberoffactors,particularlytheamountofpressuredecline.FortheConroeField,thedrive indiceshavebeencalculatedateachofthreeperiods,asgiveninlines18,19,and20ofTable7.1.For example,attheendof12months,thecalculatedinitialoilinplaceis415MMSTB,andthevalueof Np[Bt+(Rp – Rsoi)Bg]giveninline14is131MMft3.Then,fromEq.(3.11), 8 400 6 4 200 2 0 0 10 20 30 40 Production, MM STB Figure 7.3 Active oil, the Conroe Field (after Schilthuis, trans. AlME).3 50 0 Percent produced Initial oil in place, MM bbl 600 Chapter 7 206 DDI = DDI = • Saturated Oil Reservoirs N ( Bt − Bti ) N p [ Bt + ( Rp − Rsoi ) Bg ] 415 × 10 6 ( 7.46 − 7.37 ) = 0.285 131 × 10 6 SDI = NmBti ( Bg − Bgi ) Bgi N p [ Bt + ( Rp − Rsoi ) Bg ] 415 × 10 6 × 0.224 × 7.37 ) (0.00676 − 0.00637 ) 0.00637 SDI = = 0.320 131 × 10 6 WDI = (We − BwW p ) N p [ Bt + ( Rp − Rsoi ) Bg ] WDI = 51.5 × 10 6 = 0.395 131 × 10 6 These figures indicate that, during the first 12 months, 39.5% of the production was by water drive,32.0%bygas-capexpansion,and28.5%bydepletiondrive.Attheendof36months,asthe pressurestabilized,thecurrentmechanismwasessentially100%waterdriveandthecumulative mechanismincreasedto64.6%waterdrive.Iffiguresforrecoverybyeachofthethreemechanisms couldbeobtained,theoverallrecoverycouldbeestimatedusingthedriveindices.Anincreasein thedepletiondriveandgas-driveindiceswouldbereflectedbydecliningpressuresandincreasing gas-oilratiosandmightindicatetheneedforwaterinjectiontosupplementthenaturalwaterinflux andtoturntherecoverymechanismmoretowardwaterdrive. 7.3 Material Balance as a Straight Line InChapter3,section3.4,themethoddevelopedbyHavlena-Odehofapplyingthegeneralmaterial balanceequationwaspresented.4,5TheHavlena-Odehmethodisparticularlyadvantageousforuse earlyintheproductionlifeofareservoir,asitaddsconstraintsthataidinunderstandinghowthe reservoirisbehaving.Thisunderstandingallowsformoreaccuratepredictionofproductionrates, pressuredecline,andoverallrecovery.Thismethoddefinesseveralnewvariables(seeChapter3) andrewritesthematerialbalanceequationasEq.(3.13): NmBti F = NEo + N(1 + m)BtiEf,w + E g + We Bgi (3.13) 7.3 Material Balance as a Straight Line 207 Thisequationisthenreducedforaparticularapplicationandarrangedintoaformofastraight line.Whenthisisdone,theslopeandinterceptoftenyieldvaluableassistanceindeterminingsuch parametersasN and m.Theusefulnessofthisapproachisillustratedbyapplyingthemethodtothe datafromtheConroeFieldexamplediscussedinthelastsection. Forthecaseofasaturatedreservoirwithaninitialgascap,suchastheConroeField,and neglectingthecompressibilityterm,Ef,w,Eq.(3.13)becomes F = NEo + NmBti Eg + We Bgi (7.3) IfNisfactoredoutofthefirsttwotermsontheright-handsideandbothsidesoftheequationare dividedbytheexpressionremainingafterfactoring,weget F We =N+ mBti mBti Eo + Eg Eo + Eg Bgi Bgi (7.4) FortheexampleoftheConroeFieldintheprevioussection,thewaterproductionvalueswerenot known.Forthisreason,twodummyparametersaredefinedasF′ = F – WpBw and W′e = We – WpBw. Equation(7.4)thenbecomes F′ We′ =N+ mBti mBti Eo + Eg Eo + Eg Bgi Bgi (7.5) Equation(7.5)isnowinthedesiredform.IfaplotofF′/(Eo + mBtiEg/Bgi)astheordinateandW′e/(Eo + mBtiEg/Bgi)astheabscissaisconstructed,astraightlinewithslopeequalto1andinterceptequal toNisobtained.Table7.2containsthecalculatedvaluesoftheordinate,line5,andabscissa,line 7,usingtheConroeFielddatafromTable7.1.Figure7.4isaplotofthesevalues. IfaleastsquaresregressionanalysisisdoneonallthreedatapointscalculatedinTable7.2, theresultisthesolidlineshowninFig.7.4.Thelinehasaslopeof1.21andanintercept,N,of396 MMSTB.Thisslopeissignificantlylargerthan1,whichiswhatweshouldhaveobtainedfromthe Havlena-Odehmethod.Ifwenowignorethefirstdatapoint,whichrepresentstheearliestproduction,anddeterminetheslopeandinterceptofalinedrawnthroughtheremainingtwopoints(the dashedlineinFig.7.4),weget1.00foraslopeand600MMSTBforN,theintercept.Thisvalueof theslopemeetstherequirementfortheHavlena-Odehmethodforthiscase.Weshouldnowraise thequestion,canwejustifyignoringthefirstpoint?Ifwerealizethattheproductionrepresentsless than5%oftheinitialoilinplaceandthefactthatwehavemettherequirementfortheslopeof1 forthiscase,thenthereisjustificationfornotincludingthefirstpointinouranalysis.Weconclude fromouranalysisthattheinitialoilinplaceis600MMSTBfortheConroeField. Chapter 7 208 • Saturated Oil Reservoirs Table 7.2 Tabulated Values from the Conroe Field for Use in the Havlena-Odeh Method Line number Quantity Units 12 24 36 1 F′ MMft3 131 345 495 2 Eo ft3/STB 0.09 0.14 0.15 Eg ft /SCF 0.00039 0.00054 0.00056 ft3/STB 0.191 0.280 0.295 (1)/(4) MMSTB 686 1232 1678 6 W′e MMft 51.5 178 320 7 (6)/(4) MMSTB 270 636 1085 3 4 5 Eo + m Bti Bgi Months after start of production 3 Eg 3 1800 1600 F' MM STB mBti E0 + Eg Bgi 1400 1200 1000 800 600 400 200 0 200 400 600 W 'e E0 + Figure 7.4 mBti E Bgi g 800 1000 1200 MM STB Havlena-Odeh plot for the Conroe Field. Solid line represents line drawn through all data points. Dashed line represents line drawn through data points from the later production periods. 7.4 The Effect of Flash and Differential Gas Liberation Techniques 209 Thereadermaytakeissuewiththefactthatananalysiswasdoneononlytwopoints.Clearly, itwouldhavebeenbettertousemoredatapoints,butnonewereavailableinthisparticularexample.Asmoreproductiondataarecollected,thentheplotinFig.7.4canbeupdatedandthecalculationforNreviewed.TheimportantpointtorememberisthatiftheHavlena-Odehmethodisused, theconditionoftheslopeand/orinterceptmustbemetfortheparticularcasethatisbeingworked. Thisimposesanotherrestrictiononthedataandcanbeusedtojustifytheexclusionofsomedata, aswasdoneinthecaseoftheConroeFieldexample. 7.4 The Effect of Flash and Differential Gas Liberation Techniques and Surface Separator Operating Conditions on Fluid Properties Fluidpropertydataareextremelyimportantpiecesofinformationusedinreservoirengineering calculations.Itthereforebecomescrucialtobeknowledgeableaboutmethodsforobtainingthese data.Itisalsoimportanttorelatethosemethodstowhatisoccurringinthereservoirasgasevolves andthenseparatesfromtheliquidphase.Thissectioncontainsadiscussionoftwolaboratorygas liberationprocessesaswellasadiscussionoftheeffectofsurfaceseparatoroperatingpressures andtemperatures. Forheavycrudeswhosedissolvedgasesarealmostentirelymethaneandethane,themannerof separationisrelativelyunimportant.Forlightercrudesandheaviergases(i.e.,forreservoirfluidswith largerfractionsoftheintermediatehydrocarbons—mainlypropane,butanes,andpentanes),themannerofseparationraisessomeimportantquestions.Thenatureofthedifficultyliesmainlywiththese intermediate hydrocarbons that are, relatively speaking, intermediate between true gases and true liquids.Theyarethereforedividedbetweenthegasandliquidphasesinproportionsthatareaffected bythemannerofseparation.Thesituationmaybeexplainedwithreferencetotwowell-defined,isothermal,gas-liberationprocessescommonlyusedinlaboratorypressure-volume-temperature(PVT) studies.Intheflashliberationprocess,allthegasevolvedduringareductioninpressureremains in contact and presumably in equilibrium with the liquid phase from which it is liberated. In the differentialprocess,ontheotherhand,thegasevolvedduringapressurereductionisremovedfrom contactwiththeliquidphaseasrapidlyasitisliberated.Figure7.5showsthevariationofsolution gaswithpressureforthedifferentialprocessandthespecificgravityofthegasthatisbeingliberated atanypressure.Sincethespecificgravityofthegasisquiteconstantdowntoabout800psia,itcan beinferredthatveryclosetothesamequantityofgaswouldhavebeenliberatedbytheflashprocess, downto800psiaandat the same temperature.Below800psia,thevaporizationoftheintermediate hydrocarbonsbeginstobeappreciableforthefluidofFig.7.5.Inmorevolatilecrudes,itbeginsat higherpressuresandviceversa.Thevaporizationisindicatedbytheriseinthegasgravityandby theincreasingrateofgasliberation,indicatedbythesteepeningoftheslopedRso/dp.Ifallthegas liberateddownto,say,400psiaremainsincontactwiththeliquidphase,asintheflashprocess,more gasisliberatedbecausetheintermediatehydrocarbonsintheliquidphasevaporizeintotheentiregas spaceincontactwiththeliquiduntilequilibriumisreached.Becausegasisremovedasrapidlyas itisformedinthedifferentialprocess,lessvaporizationoftheintermediatesoccurs.Thereleaseof Saturated Oil Reservoirs 1200 2.0 1000 1.8 800 1.6 Differential liberation 600 Initial pressure 3480 psia Solution gas, SCF/STB • 400 200 1.4 1.2 1.0 Specific gravity of differential gas Chapter 7 210 Differential gas 0 Figure 7.5 0 400 800 1200 1600 2000 2400 Reservoir pressure, psia 2800 3200 0.8 3600 Gas solubility and gas gravity by the differential liberation process on a subsurface sample from the Magnolia Field, Arkansas (after Carpenter, Schroeder, and Cook, US Bureau of Mines).6 solutiongasatlowerpressuresbytheflashprocess,at the same temperature,isfurtheraccelerated becausethelossofmoreoftheintermediatehydrocarbonsreducesthegassolubility.Insomeflash processes,thetemperatureisreducedatsomepressureduringthegasliberationprocess,whereasdifferentialliberationsaregenerallyrunatreservoirtemperature.Becauseoftheincreasedgassolubility andthelowervolatilityoftheintermediatesatlowertemperatures,thequantityofgasreleasedbythe flashprocessisloweratthelowertemperaturesandiscommonlylessthanthequantityreleasedby thedifferentialprocessatreservoirtemperature. Table7.3givesthePVTdataobtainedfromalaboratorystudyofareservoirfluidsampleatreservoirtemperatureof220°F.Thevolumesgiveninthesecondcolumnaretheresultoftheflashgas-liberationprocessandareshownplottedinFig.7.6.Belowthebubble-pointpressureat2695psig,the volumesincludethevolumeoftheliberatedgasandarethereforetwo-phasevolumefactors.Sincethe stock-tankoilremainingatatmosphericpressuredependsonthepressure,temperature,andseparation stagesbywhichthegasisliberatedatlowerpressures,thevolumesarereportedrelativetothevolume atthebubble-pointpressure,Vb.Torelatethereservoirvolumestothestock-tankoilvolumes,additional testsareperformedonothersamplesusingsmall-scaleseparators,whichareoperatedintherangeof pressuresandtemperaturesusedinthefieldseparationofthegasandoil.Table7.4showstheresultsof fourlaboratorytestsatseparatorpressuresof0,50,100,and200psigandseparatortemperaturesfrom 74°Fto77°F.Thetemperaturesarelowerforthelowerseparatorpressuresbecauseofthegreatercoolingeffectofthegasexpansionandthegreatervaporizationoftheintermediatehydrocarboncomponents atthelowerpressures.At100psigand76°F,thetestsindicatethat505SCFareliberatedattheseparator and49SCFinthestocktank,oratotalof554SCF/STB.Thentheinitialsolutiongas-oilratio,Rsoi, is554SCF/STB.Thetestsalsoshowthat,undertheseseparationconditions,1.335bbloffluidatthe bubble-pointpressureyield1.000STBofoil.Hence,theformationvolumefactoratthebubble-point pressureis1.335bbl/STB,andthetwo-phaseflashformationvolumefactorat1773psigis 7.4 The Effect of Flash and Differential Gas Liberation Techniques 211 Btf=1.335×1.1814=1.577bbl/STB ThedatainTable7.4indicatethatbothoilgravityandrecoverycanbeimprovedbyusingan optimumseparatorpressureof100psigandbyreducingthelossofliquidcomponents,particularly theintermediatehydrocarbons,totheseparatedgas.Inreferencetomaterialbalancecalculations, Table 7.3 Reservoir Fluid Sample Tabular Data (after Kennerly, courtesy Core Laboratories, Inc.) Pressure (psig) Flash liberation at 220°F, relative volume of oil and gas (V/Vb) Differential liberation at 220°F Liberated gas-oil ratio (SCF/bbl) of residual oil Solution gas-oil ratio (SCF/bbl) of residual oil Relative oil volume (V/Vr) 5000 0.9739 1.355 4700 0.9768 1.359 4400 0.9799 1.363 4100 0.9829 1.367 3800 0.9862 1.372 3600 0.9886 1.375 3400 0.9909 1.378 3200 0.9934 1.382 3000 0.9960 1.385 2900 0.9972 1.387 2800 0.9985 1.389 2695 1.0000 2663 1.0038 2607 1.0101 0 638 1.391 42 596 1.373 89 549 1.351 150 488 1.323 152 486 1.322 213 425 1.295 1315 290 348 1.260 1010 351 287 1.232 2512 2503 1.0233 2358 1.0447 2300 2197 1.0727 2008 2000 1.1160 1773 1.1814 1702 1550 1.2691 1351 1.3792 (continued) Chapter 7 212 • Saturated Oil Reservoirs Table 7.3 Reservoir Fluid Sample Tabular Data (after Kennerly, courtesy Core Laboratories, Inc.) (continued) Pressure (psig) Flash liberation at 220°F, relative volume of oil and gas (V/Vb) Differential liberation at 220°F Liberated gas-oil ratio (SCF/bbl) of residual oil Solution gas-oil ratio (SCF/bbl) of residual oil Relative oil volume (V/Vr) 412 226 1.205 474 164 1.175 150 539 99 1.141 0 638 0 1.066 992 1.7108 711 2.2404 705 540 2.8606 410 3.7149 405 289 5.1788 Residualvolumeat60°F=1.000 Residualoilgravity=28.8°API Specificgravityofliberatedgas=1.0626 Relative volume factor, v/vb 2.5 Two phase 2.0 1.5 Saturation pressure 2695 psig 3.0 Single phase 1.0 0.5 0 1000 2000 3000 4000 5000 Pressure, psig Figure 7.6 Flash liberation PVT data for a reservoir fluid at 220°F (after Kennerly, courtesy Core Laboratories, Inc.). 7.4 The Effect of Flash and Differential Gas Liberation Techniques 213 Table 7.4 Separator Tests of Reservoir Fluid Sample (after Kennerly, courtesy Core Laboratories, Inc.) Separator pressure (psig) Separator temperature (°F) Separator Stock-tank Stock-tank Formation volume gravity gas-oil gas-oil factorb ratioa (SCF/ (°API) at ratioa 60°F (Vb/Vr) STB) (SCF/STB) 0 74 620 0 29.9 1.382 50 75 539 23 31.5 1.340 100 76 505 49 31.9 1.335 200 17 459 98 31.8 1.337 Specific gravity of flash gas air = 1.00 0.9725 Standardconditionsfor14.7psiaand60°F b Vb/Vr=barrelsofoilatthebubble-pointpressure2695psigand220°Fperstock-tankbarrelat14.7psia and60°F. a theyalsoindicatethatthevolumefactorsandsolutiongas-oilratiosdependonhowthegasand oilareseparatedatthesurface.Whendifferingseparationpracticesareusedinthevariouswells owingtooperatorpreferenceortolimitationsoftheflowingwellheadpressures,furthercomplicationsareintroduced.Figure7.7showsthevariationinoilshrinkagewithseparatorpressurefora westcentralTexasandasouthLouisianafield.Eachcrudeoilhasanoptimumseparatorpressure atwhichtheshrinkageisaminimumandstock-tankoilgravityamaximum.Forexample,inthe caseofthewestcentralTexasreservoiroil,thereisanincreasedrecoveryof7%whentheoperating separatorpressureisincreasedfromatmosphericpressureto70psig.Theeffectofusingtwostages ofseparationwiththeSouthLouisianareservoiroilisshownbythetriangle. Theeffectofchangesinseparatorpressuresandtemperaturesongas-oilratios,oilgravities,andshrinkageinreservoiroilwasdeterminedfortheScurryReefFieldbyCook,Spencer, Bobrowski,andChin.7,8Thedataobtainedfromfieldandlaboratorytestsshowedthattheamount ofgasliberatedfromtheoilproducedwasaffectedmateriallybychangesinbothseparatortemperaturesandpressures.Forexample,whentheseparatortemperaturewasreducedto62.5°F,the gas-oilratiodecreasedfrom1068SCF/STBto844SCF/STBandtheproductionincreasedfrom 125STB/dayto135STB/day.Thiswasadecreaseingas-oilratioof21%andaproductionincreaseof8%.Therefore,toyieldthesamevolumeofstock-tankoil,theproductionof8%more reservoirfluidwasneededwhentheseparatorwasoperatingatthehighertemperature. Table7.3alsogivesthesolutiongasandoilvolumefactorsforthesamereservoirfluidby differential liberationat220°F,allthewaydowntoatmosphericpressure,whereastheflashtests werestoppedat289psig,owingtolimitationsofthevolumeofthePVTcell.Figure7.8showsa plotoftheoil(liquid)volumefactorandtheliberatedgas-oilratiosrelativetoabarrelofresidual oil(i.e.,theoilremainingat1atmand60°Fafteradifferentialliberationdownto1atmat220°F). Thevolumechangefrom1.066at220°Fto1.000at60°Fisameasureofthecoefficientofthermal expansionoftheresidualoil.Insomecases,abarrelofresidualoilbythedifferentialprocessis closetoastock-tankbarrelbyaparticularflashprocess,andthetwoaretakenasequivalent.Inthe presentcase,thevolumefactoratthebubble-pointpressureis1.335bblperstock-tankbarrelby Chapter 7 214 • Saturated Oil Reservoirs 790 780 770 Barrels of stock-tank oil recovered per 1000 barrels of reservoir oil 760 750 740 730 0 20 40 60 80 Separator pressure, psig West Central Texas reservoir oil ∆500-50-0 staging 200 400 100 120 1000 1200 660 655 650 645 640 0 Figure 7.7 600 800 Separator pressure, psig South Louisiana reservoir oil Variation in stock-tank recovery with separator pressure (after Kennerly, courtesy Core Laboratories, Inc.). theflashprocess,usingseparationat100psigand76°Fversus1.391bblperresidualbarrelbythe differentialprocess.Theinitialsolutiongas-oilratiosare554SCF/STBversus638SCF/residual barrel,respectively. In addition to the volumetric data of Table 7.3, PVT studies usually obtain values for (1)thespecificvolumeofthebubble-pointoil,(2)thethermalexpansionofthesaturatedoil,and (3)thecompressibilityofthereservoirfluidatorabovethebubblepoint.ForthefluidofTable7.3,the specificvolumeofthefluidat220°Fand2695psigis0.02163ft3/lb,andthethermalexpansion is1.07741volumesat220°Fand5000psiapervolumeat74°Fand5000psia,oracoefficientof 0.00053per°F.ThecompressibilityoftheundersaturatedliquidhasbeendiscussedandcalculatedfromthedataofTable7.3inChapter2,section2.6,as10.27×10–6 psi–1between5000psia and4100psiaat220°F. 7.5 The Calculation of Formation Volume Factor and Solution Gas-Oil Ratio 215 700 500 400 1.4 300 1.3 200 1.2 100 1.1 0 Figure 7.8 0 1000 2000 3000 Pressure, psig 4000 Relative liquid volume, v/vr Gas liberated, SCF/STB of reservoir oil 600 1.0 5000 PVT data for the differential gas liberation of a reservoir fluid at 220°F (after Kennerly, courtesy Core Laboratories, Inc.). Thedeviationfactorofthegasreleasedbythedifferentialliberationprocessmaybemeasured,oritmaybeestimatedfromthemeasuredspecificgravity.Alternatively,thegascomposition maybecalculatedusingasetofvalidequilibriumconstantsandthecompositionofthereservoir fluid,andthegasdeviationfactormaybecalculatedfromthegascomposition. 7.5 The Calculation of Formation Volume Factor and Solution Gas-Oil Ratio from Differential Vaporization and Separator Tests ThedatainTables7.3and7.4canbecombinedtoyieldvaluesfortheoilformationvolumefactor andthesolutiongas-oilratio.TheformationvolumefactoriscalculatedfromEq.(7.6)or(7.7), dependingonwhetherthepressureisaboveorbelowthebubble-pointpressure:Forp>bubblepointpressure, Chapter 7 216 • Saturated Oil Reservoirs Bo = REV(Bofb) (7.6) Bofb Bo = Bod Bodb (7.7) Forp <bubble-pointpressure, where REV=RelativevolumefromtheflashliberationtestlistedinTable7.3asV/Vb Bofb=FormationvolumefactorfromseparatortestslistedinTable7.4asVb/Vr Bod=FormationvolumefactorfromdifferentialliberationtestlistedinTable7.3asV/Vr Bodb =Formationvolumefactoratthebubblepointfromdifferentialliberationtest Thesolutiongas-oilratiocanbecalculatedusingEq.(7.8), Bofb Rso = Rsofb – ( Rsofb − Rsod ) Bodb (7.8) where Rsofb=Sumofseparatorgasandthestock-tankgasfromseparatortestslistedinTable7.4 Rsod=Solutiongas-oilratiofromdifferentialliberationtestlistedinTable7.3 Rsodb =ThevalueofRsodatthebubblepoint Forexample,atapressureof5000psiaandseparatorconditionsof200psigand77°F, Bo=0.9739(1.337)=1.302bbl/STB and Rso=459+98=557SCF/STB (RecallthatRso = Rsobforpressuresabovethebubblepoint.) Atapressureof2512psig,whichisbelowthebubble-pointpressure,Bo and Rsobecome 1.337 = 1.320 bbl/STB Bo = 1.373 1.391 and 7.6 Volatile Oil Reservoirs 217 1.337 = 516 SCF/STB Rso=557– (638 − 596 ) 1.373 7.6 Volatile Oil Reservoirs Ifallgasinreservoirswasmethaneandalloilwasdecaneandheavier,thePVTpropertiesofthe reservoirfluidswouldbequitesimplebecausethequantitiesofoilandgasobtainedfromamixture ofthetwowouldbealmostindependentofthetemperatures,thepressures,andthetypeofthegas liberationprocessbywhichthetwoareseparated.Lowvolatilitycrudesapproachthisbehavior, whichisapproximatelyindicatedbyreservoirtemperaturesbelow150°F,solutiongas-oilratios below500SCF/STB,andstock-tankgravitiesbelow35°API.Becausethepropane,butane,and pentanecontentofthesefluidsislow,thevolatilityislow. Fortheconditionslistedpreviously,butnottoofarabovetheapproximatelimitsoflowvolatilityfluids,satisfactoryPVTdataformaterialbalanceuseareobtainedbycombiningseparator testsatappropriatetemperaturesandpressureswiththeflashanddifferentialtestsaccordingto theprocedurediscussedintheprevioussection.Althoughthisprocedureissatisfactoryforfluids ofmoderatevolatility,itbecomeslesssatisfactoryasthevolatilityincreases;morecomplicated, extensive,andpreciselaboratorytestsarenecessarytoprovidePVTdatathatarerealisticinthe application,particularlytoreservoirsofthedepletiontype. Withpresent-daydeeperdrilling,manyreservoirsofhighervolatilityarebeingdiscovered thatincludethegas-condensatereservoirsdiscussedinChapter5.Thevolatilityishigherbecause ofthehigherreservoirtemperaturesatdepth,approaching500°Finsomecases,andalsobecause ofthecompositionofthefluids,whicharehighinpropanethroughdecane.Thevolatile oil reservoirisrecognizedasatypeintermediateinvolatilitybetweenthemoderatelyvolatilereservoir andthegas-condensatereservoir.JacobyandBerryhaveapproximatelydefinedthevolatiletype ofreservoirasonecontainingrelativelylargeproportionsofethanethroughdecaneatareservoir temperaturenearorabove250°F,withahighformationvolumefactorandstock-tankoilgravity above45°API.9ThefluidoftheElkCityField,Oklahoma,isanexample.Thereservoirfluidatthe initialpressureof4364psiaandreservoirtemperatureof180°Fhadaformationvolumefactorof 2.624bbl/STBandasolutiongas-oilratioof2821SCF/STB,bothrelativetoproductionthrough asingleseparatoroperatingat50psigand60°F.Thestock-tankgravitywas51.4°APIforthese separatorconditions.Cook,Spencer,andBobrowskidescribedtheElkCityFieldandatechnique forpredictingrecoverybydepletiondriveperformance.10ReudelhuberandHindsandJacobyand Berryalsodescribedsomewhatsimilarlaboratorytechniquesandpredictionmethodsforthedepletiondriveperformanceofthesevolatileoilreservoirs.11,9Themethodsaresimilartothoseused forgas-condensatereservoirsdiscussedinChapter5. Atypicallaboratorymethodofestimatingtherecoveryfromvolatilereservoirsisasfollows.Samplesofprimaryseparatorgasandliquidareobtainedandanalyzedforcomposition. Withthesecompositionsandaknowledgeofseparatorgasandoilflowrates,thereservoirfluid compositioncanbecalculated.Also,byrecombiningtheseparatorfluidsintheappropriateratio,areservoirfluidsamplecanbeobtained.ThisreservoirfluidsampleisplacedinaPVTcell Chapter 7 218 • Saturated Oil Reservoirs andbroughttoreservoirtemperatureandpressure.Atthispoint,severaltestsareconducted.A constantcompositionexpansionisperformedtodeterminerelativevolumedata.Thesedataare theflashliberationvolumedatalistedinTable7.3.Onaseparatereservoirsample,aconstant volumeexpansionisperformedwhilethevolumesandcompositionsoftheproducedphasesare monitored.Theproducedphasesarepassedthroughaseparatorsystemthatsimulatesthesurface facilities.Byexpandingtheoriginalreservoirfluidfromtheinitialreservoirpressuredownto anabandonmentpressure,theactualproductionprocessfromthereservoirissimulated.Using thedatafromthelaboratoryexpansion,thefieldproductioncanbeestimatedwithaprocedure similartotheoneusedinExample5.3topredictperformancefromagas-condensatereservoir. 7.7 Maximum Efficient Rate (MER) Manystudiesindicatethattherecoveryfromtruesolutiongas-drivereservoirsbyprimarydepletionisessentiallyindependentofbothindividualwellratesandtotalorreservoirproductionrates. Keller,Tracy,andRoeshowedthatthisistrueevenforreservoirswithseverepermeabilitystratificationwherethestrataareseparatedbyimpermeablebarriersandarehydraulicallyconnected onlyatthewells.12TheGloyd-MitchellzoneoftheRodessaField(seeChapter6,section6.5)is anexampleofasolutiongas-drivereservoirthatisessentiallynotrate sensitive(i.e.,therecovery isunrelatedtotherateatwhichthereservoirisproduced).Therecoveryfromverypermeable, uniformreservoirsunderveryactivewaterdrivesmayalsobeessentiallyindependentoftherates atwhichtheyareproduced. Manyreservoirsareclearlyrate sensitiveand,forthisreason,manygoverningbodieshave imposedallowablesthatlimittheproductiontoaspecifiedrateinordertoensureamaximumoverallrecoveryofthewell.Theseallowablesarenottypicallyreservoirspecificandinconventional fieldsmayberestrictive.Reservoirengineerscancalculateamaximum efficient rate(MER)fora specificreservoir.Productionatorbelowthisratewillyieldamaximumultimaterecovery,while productionabovethisratewillresultinasignificantreductioninthepracticalultimateoilrecovery.13,14GoverningbodieshavebeenknowntoadjustallowablesforareservoirwhenanMERhas beenproven. Rate-sensitivereservoirsimplythatthereissomemechanism(s)atworkinthereservoirthat, inapracticalperiod,cansubstantiallyimprovetherecoveryoftheoilinplace.Thesemechanisms include(1)partialwaterdrive,(2)gravitationalsegregation,and(3)thoseeffectiveinreservoirsof heterogeneouspermeability. Wheninitiallyundersaturatedreservoirsareproducedunderpartialwaterdriveatvoidage rates(gas,oil,andwater)considerablyinexcessofthenaturalinfluxrate,theyareproducedessentiallyassolutiongas-drivereservoirsmodifiedbyasmallwaterinflux.Assumingthatrecovery bywaterdisplacementisconsiderablylargerthanrecoverybysolutiongasdrive,therewillbea considerablelossinrecoverableoilbythehighproductionrate,evenwhentheoilzoneiseventuallyentirelyinvadedbywater.Thelossiscausedbytheincreaseintheviscosityoftheoil,the decreaseinthevolumefactoroftheoilatlowerpressures,andtheearlierabandonmentofthewells thatmustbeproducedbyartificiallift.Becauseofthehigheroilviscosityatthelowerpressure, 7.7 Maximum Efficient Rate (MER) 219 producingwater-oilratioswillbehigher,andtheeconomiclimitofproductionratewillbereached atloweroilrecoveries.Becauseoftheloweroilvolumefactoratthelowerpressure,atthesame residualoilsaturationintheinvadedarea,morestock-tankoilwillbeleftatlowpressure.There are,ofcourse,additionalbenefitstoberealizedbyproducingatsucharatesoastomaintainhigh reservoirpressure.Ifthereisnoappreciablegravitationalsegregationandtheeffectsofreservoir heterogeneityaresmall,thentheMERforapartialwater-drivereservoircanbeinferredfroma studyoftheeffectofthenetreservoirvoidagerateonreservoirpressureandtheconsequenteffect ofpressureonthegassaturationrelativetothecriticalgassaturation(i.e.,ongas-oilratios).The MERmayalsobeinferredfromstudiesofthedriveindices(Eq.[7.3]).Thepresenceofagascap inapartialwater-drivefieldintroducescomplicationsindeterminingtheMER,whichisaffected bytherelativesizeofthegascapandtherelativeefficienciesofoildisplacementbytheexpanding gascapandbytheencroachingwater. TheGloyd-MitchellzoneoftheRodessaFieldwasnotratesensitivebecausetherewasno waterinfluxandbecausetherewasessentiallynogravitationalsegregationofthefreegasreleased fromsolutionandtheoil.Iftherehadbeensubstantialsegregation,thewellcompletionandwell workovermeasures,whichweretakeninanefforttoreducegas-oilratios,wouldhavebeeneffective,astheyareinmanysolutiongas-drivereservoirs.Insomecases,agascapformsinthehigher portionsofthereservoir,andwhenhighgas-oilratiowellsarepenalizedorshutin,theremaybe asubstantialimprovementinrecovery,asindicatedbyEq.(7.11),forareductioninthevalueof theproducedgas-oilratioRp.Undertheseconditions,theMERisthatrateatwhichgravitational segregationissubstantialforpracticalproducingrates. Gravitational segregation is also important in many gas-cap reservoirs. The effect of displacementrateonrecoverybygas-capexpansionwhenthereissubstantialsegregationoftheoil andgasisdiscussedinChapter10.ThestudiespresentedontheMileSixPoolshowthat,atthe adopteddisplacementrate,therecoverywillbeapproximately52.4%.Ifthedisplacementrateis doubled,therecoverywillbereducedtoabout36.0%,andatveryhighrates,itwilldropto14.4% fornegligiblegravitysegregation. Gravitationalsegregationalsooccursinthedisplacementofoilbywater,andlikethegas-oil segregation,itisalsodependentonthetimefactor.Gravitysegregationisgenerallyoflessrelative importance in water drive than in gas-cap drive because of the much higher recoveries usually obtainedbywaterdrive.TheMERforwater-drivereservoirsisthatrateabovewhichtherewillbe insufficienttimeforeffectivesegregationand,therefore,asubstantiallossofrecoverableoil.The ratemaybeinferredfromcalculationssimilartothoseusedforgasdisplacementinChapter10or fromlaboratorystudies.Itisinterestingthat,inthecaseofgravitationalsegregation,thereservoir pressureisnottheindexoftheMER.Inanactivewater-drivefield,forexample,theremaybeno appreciabledifferenceinthereservoirpressuredeclineforaseveralfoldchangeintheproduction rate,andyetrecoveryatthelowerratemaybesubstantiallyhigherifgravitysegregationiseffectiveatthelowerratebutnotatthehigher. Aswaterinvadesareservoirofheterogeneouspermeability,thedisplacementismorerapid in the more permeable portions, and considerable quantities of oil may be bypassed if the 220 Chapter 7 • Saturated Oil Reservoirs displacementrateistoohigh.Atlowerrates,thereistimeforwatertoenterthelesspermeable portionsoftherockandrecoveralargerportionoftheoil.Asthewaterlevelrises,waterissometimesimbibedordrawnintothelesspermeableportionsbycapillaryaction,andthismayalsohelp recoveroilfromthelesspermeableareas.Becausewaterimbibitionsandtheconsequentcapillary expulsionofoilarefarfrominstantaneous,ifappreciableadditionaloilcanberecoveredbythis mechanism,thedisplacementrateshouldbeloweredifpossible.AlthoughtheMERunderthese circumstances is more difficult to establish, it may be inferred from the degree of the reservoir heterogeneityandthecapillarypressurecharacteristicsofthereservoirrocks. InthepresentdiscussionofMER,itisrealizedthattherecoveryofoilisalsoaffectedbythe reservoirmechanisms,fluidinjection,gas-oilandwater-oilratiocontrol,andotherfactorsandthat itisdifficulttospeakofrate-sensitivemechanismsentirelyindependentlyoftheseotherfactors, whichinmanycasesarefarmoreimportant. Problems 7.1 CalculatethevaluesforthesecondandfourthperiodsthroughthefourteenthstepofTable7.1 fortheConroeField. 7.2 CalculatethedriveindicesattheConroeFieldforthesecondandfourthperiods. 7.3 IftherecoverybywaterdriveattheConroeFieldis70%,bysegregationdrive50%,andby depletiondrive25%,usingthedriveindicesforthefifthperiod,calculatetheultimateoil recoveryexpectedattheConroeField. 7.4 ExplainwhythefirstmaterialbalancecalculationattheConroeFieldgivesalowvaluefor theinitialoilinplace. 7.5 (a) C alculate the single-phase formation volume factor on a stock-tank basis, from the PVTdatagiveninTables7.3and7.4atareservoirpressureof1702psig,forseparator conditionsof100psigand76°F. (b) CalculatethesolutionGORat1702psigonastock-tankbasisforthesameseparator conditions. (c) Calculatethetwo-phaseformationvolumefactorbyflashseparationat1550psigfor separatorconditionsof100psigand76°F. 7.6 Fromthecoredatathatfollow,calculatetheinitialvolumeofoilandfreegasinplaceby thevolumetricmethod.Then,usingthematerialbalanceequation,calculatethecubicfeet ofwaterthathaveencroachedintothereservoirattheendofthefourperiodsforwhich productiondataaregiven. Problems 221 Pressure (psia) Bt (bbl/STB) Bg (ft3/SCF) NP (STB) RP (SCF/STB) WP (STB) 3480 1.4765 0.0048844 0 0 0 3190 1.5092 0.0052380 11.17MM 885 224.5M 3139 1.5159 0.0053086 13.80MM 884 534.2M 3093 1.5223 0.0053747 16.41MM 884 1005.0M 3060 1.5270 0.0054237 18.59MM 896 1554.0M Averageporosity=16.8% Connatewatersaturation=27% Productiveoilzonevolume=346,000ac-ft Productivegaszonevolume=73,700ac-ft Bw=1.025bbl/STB Reservoirtemperature=207°F Initialreservoirpressure=3480psia 7.7 ThefollowingPVTdataarefortheAnethFieldinUtah: Pressure (psia) Bo (bbl/STB) Rso (SCF/STB) 2200 1.383 727 1850 1.388 1600 1.358 1300 Bg (bbl/SCF) μo/μg 727 0.00130 35 654 0.00150 39 1.321 563 0.00182 47 1000 1.280 469 0.00250 56 700 1.241 374 0.00375 68 400 1.199 277 0.00691 85 100 1.139 143 0.02495 130 40 1.100 78 0.05430 420 Theinitialreservoirtemperaturewas133°F.Theinitialpressurewas2200psia,andthe bubble-pointpressurewas1850psia.Therewasnoactivewaterdrive.From1850psiato 1300psia,atotalof720MMSTBofoiland590.6MMMSCFofgaswasproduced. (a) Howmanyreservoirbarrelsofoilwereinplaceat1850psia? (b) Theaverageporositywas10%,andconnatewatersaturationwas28%.Thefieldcovered50,000acres.Whatistheaverageformationthicknessinfeet? Chapter 7 222 • Saturated Oil Reservoirs 7.8 Youhavebeenaskedtoreviewtheperformanceofacombinationsolutiongas,gas-capdrive reservoir.Welltestandloginformationshowthatthereservoirinitiallyhadagascaphalfthe sizeoftheinitialoilvolume.Initialreservoirpressureandsolutiongas-oilratiowere2500 psiaand721SCF/STB,respectively.Usingthevolumetricapproach,initialoilinplacewas foundtobe56MMSTB.Asyouproceedwiththeanalysis,youdiscoverthatyourbosshas notgivenyouallthedatayouneedtomaketheanalysis.Themissinginformationisthat,at somepointinthelifeoftheproject,apressuremaintenanceprogramwasinitiatedusinggas injection.Thetimeofthegasinjectionandthetotalamountofgasinjectedarenotknown. Therewasnoactivewaterdriveorwaterproduction.PVTandproductiondataareinthe followingtable: Pressure (psia) Bg (bbl/STB) Bt (bbl/SCF) NP (STB) RP (SCF/STB) 2500 0.001048 1.498 0 0 2300 0.001155 1.523 3.741MM 716 2100 0.001280 1.562 6.849MM 966 1900 0.001440 1.620 9.173MM 1297 1700 0.001634 1.701 10.99MM 1623 1500 0.001884 1.817 12.42MM 1953 1300 0.002206 1.967 14.39MM 2551 1100 0.002654 2.251 16.14MM 3214 900 0.003300 2.597 17.38MM 3765 700 0.004315 3.209 18.50MM 4317 500 0.006163 4.361 19.59MM 4839 (a) Atwhatpoint(i.e.,pressure)didthepressuremaintenanceprogrambegin? (b) HowmuchgasinSCFhadbeeninjectedwhenthereservoirpressurewas500psia?Assumethatthereservoirgasandtheinjectedgashavethesamecompressibilityfactor. 7.9 Anoilreservoirinitiallycontains4MMSTBofoilatitsbubble-pointpressureof3150psia, with600SCF/STBofgasinsolution.Whentheaveragereservoirpressurehasdroppedto 2900psia,thegasinsolutionis550SCF/STB.Boiwas1.34bbl/STBandBoatapressureof 2900psiais1.32bbl/STB. Someadditionaldataareasfollows: Rp=600SCF/STBat2900psia Swi=0.25 Bg=0.0011bbl/SCFat2900psia Thisisavolumetricreservoir. Thereisnooriginalgascap. Problems 223 (a) HowmanySTBofoilwillbeproducedwhenthepressurehasdecreasedto2900psia? (b) Calculatethefreegassaturationthatexistsat2900psia. 7.10 Giventhefollowingdatafromlaboratorycoretests,productiondata,andlogginginformation,calculatethewaterinfluxandthedriveindicesat2000psia: Wellspacing=320ac Netpaythickness=50ftwiththegas/oilcontact10ftfromthetop Porosity=0.17 Overallinitialwatersaturationinthenetpay=0.26 Overallinitialgassaturationinthenetpay=0.15 Bubble-pointpressure=3600psia Initialreservoirpressure=3000psia Reservoirtemperature=120°F Boi=1.26bbl/STB Bo=1.37bbl/STBatthebubble-pointpressure Bo=1.19bbl/STBat2000psia Np=2.0MMSTBat2000psia Gp=2.4MMMSCFat2000psia Gascompressibilityfactor,z=1.0–0.0001p Solutiongas-oilratio,Rso=0.2p 7.11 Fromthefollowinginformation,determine (a) Cumulativewaterinfluxatpressures3625,3530,and3200psia (b) Water-driveindexforthepressuresin(a) Bg (bbl/SCF) Rso (SCF/ STB) Bt (bbl/ STB) 0 0.000892 888 1.464 0.49MM 0 0.000895 884 1.466 0.36MM 2.31MM 0.001MM 0.000899 880 1.468 3585 0.79MM 4.12MM 0.08MM 0.000905 874 1.469 3530 1.21MM 5.68MM 0.26MM 0.000918 860 1.476 3460 1.54MM 7.00MM 0.41MM 0.000936 846 1.482 3385 2.08MM 8.41MM 0.60MM 0.000957 825 1.491 3300 2.58MM 9.71MM 0.92MM 0.000982 804 1.501 3200 3.40MM 11.62MM 1.38MM 0.001014 779 1.519 Pressure (psia) Np (STB) GP (SCF) WP (STB) 3640 0 0 3625 0.06MM 3610 Chapter 7 224 • Saturated Oil Reservoirs 7.12 Thecumulativeoilproduction,Np,andcumulativegasoilratio,Rp,asfunctionsoftheaveragereservoirpressureoverthefirst10yearsofproductionforagas-capreservoir,areas follows.UsetheHavlena-Odehapproachtosolvefortheinitialoilandgas(bothfreeand solution)inplace. Pressure (psia) Np (STB) RP (SCF/ STB) Bo (bbl/ STB) Ro (SCF/STB) Bg (bbl/STB) 3330 0 0 1.2511 510 0.00087 3150 3.295MM 1050 1.2353 477 0.00092 3000 5.903MM 1060 1.2222 450 0.00096 2850 8.852MM 1160 1.2122 425 0.00101 2700 11.503MM 1235 1.2022 401 0.00107 2550 14.513MM 1265 1.1922 375 0.00113 2400 17.730MM 1300 1.1822 352 0.00120 7.13 Usingthefollowingdata,determinetheoriginaloilinplacebytheHavlena-Odehmethod.Assumethereisnowaterinfluxandnoinitialgascap.Thebubble-pointpressureis 1800psia. Pressure (psia) Np (STB) RP (SCF/ STB) Bt (bbl/ STB) Rso (SCF/STB) Bg (bbl/SCF) 1800 0 0 1.268 577 0.00097 1482 2.223MM 634 1.335 491 0.00119 1367 2.981MM 707 1.372 460 0.00130 1053 5.787MM 1034 1.540 375 0.00175 References Petroleum Reservoir Efficiency and Well Spacing,StandardOilDevelopmentCompany,1934,24. SylvainJ.Pirson,Elements of Oil Reservoir Engineering,2nded.,McGraw-Hill,1958,635–93. RalphJ.Schilthuis,“ActiveOilandReservoirEnergy,”Trans.AlME(1936),118,33. D.HavlenaandA.S.Odeh,“TheMaterialBalanceasanEquationofaStraightLine,”Jour. of Petroleum Technology(Aug.1963),896–900. 5. D. Havlena and A. S. Odeh, “The Material Balance as an Equation of a Straight Line: PartII—FieldCases,”Jour. of Petroleum Technology(July1964),815–22. 6. Charles B. Carpenter, H. J. Shroeder, andAlton B. Cook, “Magnolia Oil Field, Columbia County,Arkansas,”USBureauofMines,R.I.3720,1943,46,47,82. 1. 2. 3. 4. References 225 7. AltonB.Cook,G.B.Spencer,F.P.Bobrowski,andTimChin,“ChangesinGas-OilRatios withVariationsinSeparatorPressuresandTemperatures,”Petroleum Engineer(Mar.1954), 26,B77–B82. 8. AltonB.Cook,G.B.Spencer,F.P.Bobrowski,andTimChin,“ANewMethodofDeterminingVariationsinPhysicalPropertiesinaReservoir,withApplicationtotheScurryReefField, ScurryCounty,Texas,”USBureauofMines,R.I.5106,Feb.1955,10–11. 9. R.H.JacobyandV.J.BerryJr.,“AMethodforPredictingDepletionPerformanceofaReservoirProducingVolatileCrudeOil,”Trans.AlME(1957),201,27. 10. AltonB.Cook,G.B.Spencer,andF.P.Bobrowski,“SpecialConsiderationsinPredictingReservoirPerformanceofHighlyVolatileTypeOilReservoirs,”Trans.AlME(1951),192,37–46. 11. F.O.ReudelhuberandRichardF.Hinds,“ACompositionalMaterialBalanceMethodforPredictionofRecoveryfromVolatileOilDepletionDriveReservoirs,”Trans.AlME(1957),201, 19–26. 12. W.O.Keller,G.W.Tracy,andR.P.Roe,“EffectsofPermeabilityonRecoveryEfficiencyby GasDisplacement,”Drilling and Production Practice,API(1949),218. 13. EdgarKraus,“MER—AHistory,”Drilling and Production Practice,API(1947),108–10. 14. StewartE.Buckley,Petroleum Conservation,AmericanInstituteofMiningandMetallurgical Engineers,1951,151–63. This page intentionally left blank C H A P T E R 8 Single-Phase Fluid Flow in Reservoirs 8.1 Introduction Inthepreviousfourchapters,thematerialbalanceequationsforeachofthefourreservoirtypesdefinedinChapter1weredeveloped.Thesematerialbalanceequationsmaybeusedtocalculatethe productionofoiland/orgasasafunctionofreservoirpressure.Thereservoirengineer,however, wouldliketoknowtheproductionasafunctionoftime.Tolearnthis,itisnecessarytodevelopa modelcontainingtimeorsomerelatedproperty,suchasflowrate. ThischaptercontainsadetaileddiscussionofDarcy’slawasitappliestohydrocarbonreservoirs.Thediscussionwillconsiderfourmajorinfluencesonfluidflow,theireffectonthereservoir fluid,andthemanipulationofDarcy’slawtoaccountfortheseinfluences.Thefirstmajorinfluence isthenumberofphasespresent.Thischapterwillconsideronlysingle-phaseflowregimes.Subsequentchapterswillinvestigatespecificapplicationsofmultiphaseflow.Thesecondmajorinfluence isthecompressibilityofthefluid.Thirdisthegeometryoftheflowsystem,namelylinear,radial, orsphericalflow.Fourthisthetimedependenceoftheflowsystem.Steadystatewillbeconsidered first,followedbytransient,late-transient,andpseudosteadystate.Thechapterconcludeswithan introductiontopressuretransienttestingmethodsthataidthereservoirengineeringettinginformationsuchasaveragepermeability,damagearoundawellbore,anddrainageareaofaparticular productionwell. 8.2 Darcy’s Law and Permeability In1856,asaresultofexperimentalstudiesontheflowofwaterthroughunconsolidatedsandfilter beds,HenryDarcyformulatedthelawthatbearshisname.Thislawhasbeenextendedtodescribe, withsomelimitations,themovementofotherfluids,includingtwoormoreimmisciblefluids,in consolidatedrocksandotherporousmedia.Darcy’slawstatesthatthevelocityofahomogeneous 227 Chapter 8 228 • Single-Phase Fluid Flow in Reservoirs fluidinaporousmediumisproportionaltothedrivingforceandinverselyproportionaltothefluid viscosity,or υ = − 0.001127 k dp − 0.433γ ′ cos α μ ds (8.1) where υ=theapparentvelocity,bbl/day-ft2 k=permeability,millidarcies(md) μ=fluidviscosity,cp p=pressure,psia s=distancealongflowpathinft γ ′=fluidspecificgravity(alwaysrelativetowater) α=theanglemeasuredcounterclockwisefromthedownwardverticaltothepositives direction andtheterm dp ds − 0.433 γ ′ cos α representsthedrivingforce.Thedrivingforcemaybecausedbyfluidpressuregradients(dp/ds) and/orhydraulic(gravitational)gradients(0.433γ ′ cosα).Inmanycasesofpracticalinterest,the hydraulicgradients,althoughalwayspresent,aresmallcomparedwiththefluidpressuregradients andarefrequentlyneglected.Inothercases,notablyproductionbypumpingfromreservoirswhose pressureshavebeendepletedandgas-capexpansionreservoirswithgoodgravitydrainagecharacteristics,thehydraulicgradientsareimportantandmustbeconsidered. Theapparentvelocity, υ,isequaltoqB/A,whereqisthevolumetricflowrateinSTB/day, Bistheformationvolumefactor,andAistheapparentortotalareaofthebulkrockmaterialinsquare feetperpendiculartotheflowdirection.Aincludestheareaofthesolidrockmaterialaswellasthe areaoftheporechannels.Thefluidpressuregradient,dp/ds,istakeninthesamedirectionasυ and q.Thenegativesigninfrontoftheconstant0.001127indicatesthatiftheflowistakenaspositivein thepositives-direction,thenthepressuredecreasesinthatdirection,sotheslopedp/dsisnegative. Darcy’slawappliesonlyintheregionoflaminarflowcharacterizedbylowfluidvelocities; inturbulentflow,whichoccursathighfluidvelocities,thepressuregradientisdependentonthe flowratebutusuallyincreasesatagreaterratethandoestheflowrate.Fortunately,Darcy’slawis validforliquidflow,exceptforsomeinstancesofquitelargeproductionorinjectionratesinthe vicinityofthewellbore,theflowinthereservoir,andmostlaboratorytests.However,gasflowing nearthewellboreislikelytobesubjecttonon-Darcyflow.Darcy’slawdoesnotapplytoflowwithinindividualporechannelsbuttoportionsofarock,thedimensionsofwhicharereasonablylarge 8.2 Darcy’s Law and Permeability 229 comparedwiththesizeoftheporechannels.Inotherwords,itisastatisticallawthataveragesthe behaviorofmanyporechannels.Forthisreason,althoughsampleswithdimensionsofacentimeter ortwoaresatisfactoryforpermeabilitymeasurementsonuniformsandstones,muchlargersamples arerequiredforreliablemeasurementsoffractureandvugular-typerocks. Owingtotheporosityoftherock,thetortuosityoftheflowpaths,andtheabsenceofflowin someofthe(dead)porespaces,theactualfluidvelocitywithinporechannelsvariesfrompointto pointwithintherockandmaintainsanaveragethatismanytimestheapparentbulkvelocity.Because actual velocities are in general not measurable, and to keep porosity and permeability separated, apparentvelocityformsthebasisofDarcy’slaw.Thismeanstheactualaverageforwardvelocityof afluidistheapparentvelocitydividedbytheporositywherethefluidcompletelysaturatestherock. Abasicunitofpermeabilityisthedarcy(d).Arockof1-dpermeabilityisoneinwhichafluidof1-cpviscositywillmoveatavelocityof1cm/secunderapressuregradientof1atm/cm.Since thisisafairlylargeunitformostproducingrocks,permeabilityiscommonlyexpressedinunits onethousandthaslarge,themillidarcy,or0.001d.Throughoutthistext,theunitofpermeability usedisthemillidarcy(md).Conventionaloilandgassandshavepermeabilitiesvaryingfromafew millidarcies to several thousands. Intergranular limestone permeabilities may be only a fraction ofamillidarcyandyetbecommercialiftherockcontainsadditionalnaturalorartificialfractures orotherkindsofopenings.Fracturedandvugularrocksmayhaveenormouspermeabilities,and somecavernouslimestonesapproachtheequivalentofundergroundtanks.Inrecentyears,unconventionalreservoirshavebeendevelopedwithpermeabilitiesinthemicrodarcy(1μd=10–6d)or evennanodarcy(1nd=10–9d)range. Thepermeabilityofasampleasmeasuredinthelaboratorymayvaryconsiderablyfromthe averageofthereservoirasawholeoraportionthereof.Thereareoftenwidevariationsbothlaterallyandvertically,withthepermeabilitysometimeschangingseveralfoldwithinaninchinrock thatappearsquiteuniform.Generally,thepermeabilitymeasuredparalleltothebeddingplanesof stratifiedrocksislargerthantheverticalpermeability.Also,insomecases,thepermeabilityalong thebeddingplanevariesconsiderablyandconsistentlywithcoreorientation,owingpresumably totheorienteddepositionofmoreorlesselongatedparticlesand/orthesubsequentleachingor cementing action of migrating waters. Some reservoirs show general permeability trends from oneportiontoanother,andmanyreservoirsareclosedonallorpartoftheirboundariesbyrockof verylowpermeability,certainlybytheoverlyingcaprock.Theoccurrenceofoneormorestrataof consistentpermeabilityoveraportionorallofareservoiriscommon.Intheproperdevelopment ofreservoirs,itiscustomarytocoreselectedwellsthroughouttheproductiveareameasuringthe permeabilityandporosityoneachfootofcorerecovered.Theresultsarefrequentlyhandledstatistically.1,2Inveryheterogeneousreservoirs,especiallycarbonates,itmaybethatnocoreisretrieved fromthemostproductiveintervalsbecausetheyarehighlyfracturedorevenrubblized.Forsuch reservoirscore-derivedpermeabilitystatisticsmaybeveryconservativeorevenmisleadinglylow. Hydraulic gradients in reservoirs vary from a maximum near 0.500 psi/ft for brines to 0.433psi/ftforfreshwaterat60°F,dependingonthepressure,temperature,andsalinityofthewater.Reservoiroilsandhigh-pressuregasandgas-condensategradientslieintherangeof0.10–0.30 psi/ft,dependingonthetemperature,pressure,andcompositionofthefluid.Gasesatlowpressure Chapter 8 230 • Single-Phase Fluid Flow in Reservoirs willhaveverylowgradients(e.g.,about0.002psi/ftfornaturalgasat100psia).Thefiguresgiven aretheverticalgradients.Theeffectivegradientisreducedbythefactorcos α.Thusareservoir oilwithareservoirspecificgravityof0.60willhaveaverticalgradientof0.260psi/ft;however,if thefluidisconstrainedtoflowalongthebeddingplaneofitsstratum,whichdipsat15°(α=75°), thentheeffectivehydraulicgradientisonly0.26cos75°,or0.067psi/ft.Althoughthesehydraulic gradientsaresmallcomparedwithusualreservoirpressures,thefluidpressuregradients,exceptin thevicinityofwellbores,arealsoquitesmallandinthesamerange.Fluidpressuregradientswithin afewfeetofwellboresmaybeashighastensofpsiperfootduetotheflowintothewellborebut willfalloffrapidlyawayfromthewell,inverselywiththeradius. Frequently,staticpressuresmeasuredfromwelltestsarecorrectedtothetopoftheproduction (perforated)intervalwithaknowledgeofthereservoirfluidgradient.Theyalsocanbeadjustedto acommondatumlevelforagivenreservoirbyusingthesamereservoirfluidgradient.Example8.1 showsthecalculationofapparentvelocitybytwomethods.Thefirstisbycorrectingthewellpressurestothedatumlevelusinginformationabouthydraulicgradients.ThesecondisbyusingEq.(8.1). Example 8.1 Calculating Datum Level Pressures, Pressure Gradients, and Reservoir Flow from Static Pressure Measurements in Wells Given Distancebetweenwells(seeFig.8.1) Truestratumthickness=20ft Dipofstratumbetweenwells=8°37′ Well no. 1 Well no. 2 1320 ft Top perf. 7520 ft 3380 psia Datum 7600 ft 20 ft Top perf. 7720 ft 3400 psia Figure 8.1 Dip = 8º37' Cross section between the two wells of Example 8.1. Note exaggerated vertical scale. 8.2 Darcy’s Law and Permeability 231 Reservoirdatumlevel=7600ftsubsea Reservoirfluidspecificgravity=0.693(water=1.00) Reservoirpermeability=145md Reservoirfluidviscosity=0.32cp Wellnumber1staticpressure=3400psiaat7720ftsubsea Wellnumber2staticpressure=3380psiaat7520ftsubsea First Solution Reservoirfluidgradient=Reservoirfluidspecificgravity ×Hydraulicgradientfreshwater=0.693×0.433=0.300psi/ft p1at7600ftdatum=Wellnumber1staticpressure –(Elevationdifferenceofwellnumber1anddatum ×Reservoirfluidgradient)=3400–120×0.30=3364psia p2at7600ftdatum=Wellnumber2staticpressure +(Elevationdifferenceofwellnumber2anddatum ×Reservoirfluidgradient)=3380+80×0.30=3404psia Thedifferenceof40psiindicatesthatfluidismovingdowndip,fromwell2towell1.The averageeffectivegradientis40/1335=0.030psi/ft,where1335isthedistancealongthestratum betweenthewells.Thevelocitythenis v=0.001127×(Reservoirpermeability/ Reservoirfluidviscosity)×Averageeffectivegradient v = 0.001127 × 0.145 × 0.030 = 0.0153bbl/day/ft 2 0.32 Second Solution Takethepositivedirectionfromwell1towell2.Thenα=98°37′andcosα=–0.1458. v = − 0.001127 v=− k dp − 0.433γ ′ cos α μ ds 0.001127 × 0.145 ( 3380 − 3400 ) − 0.433 × 0.693 × ( −0.1458 ) 0.32 1335 Chapter 8 232 • Single-Phase Fluid Flow in Reservoirs v=–0.0153bbl/day/sqft Thenegativesignindicatesthatfluidisflowinginthenegativedirection(i.e.,fromwell2towell1). Equation(8.1)suggeststhatthevelocityandpressuregradientarerelatedbythemobility. Themobility,giventhesymbolλ,istheratioofpermeabilitytoviscosity,k/μ.Themobilityappears inallequationsdescribingtheflowofsingle-phasefluidsinreservoirrocks.Whentwofluidsare flowingsimultaneously—forexample,gasandoiltoawellbore,itistheratioofthemobilityofthe gas, λg,tothatoftheoil,λo,thatdeterminestheirindividualflowrates.ThemobilityratioM(see Chapter10)isanimportantfactoraffectingthedisplacementefficiencyofoilbywater.Whenone fluiddisplacesanother,thestandardnotationforthemobilityratioisthemobilityofthedisplacing fluidtothatofthedisplacedfluid.Forwater-displacingoil,itisλw/λo. 8.3 The Classification of Reservoir Flow Systems Reservoirflowsystemsareusuallyclassedaccordingto(1)thecompressibilityoffluid,(2)the geometryofthereservoirorportionthereof,and(3)therelativerateatwhichtheflowapproaches asteady-stateconditionfollowingadisturbance. For most engineering purposes, the reservoir fluid may be classed as (1) incompressible, (2)slightlycompressible,or(3)compressible.Theconceptoftheincompressiblefluid,thevolume ofwhichdoesnotchangewithpressure,simplifiesthederivationandthefinalformofmanyequations.However,theengineershouldrealizethattherearenotrulyincompressiblefluids. A slightly compressible fluid, which is the description of nearly all liquids, is sometimes definedasonewhosevolumechangewithpressureisquitesmallandexpressiblebytheequation V = VR ec ( pR − p ) (8.2) where R = reference conditions TheexponentialterminEq.(8.2)canbeexpandedandapproximated,duetothetypically smallvalueofc(pR – p),toyieldthefollowing: V = VR [1 + c(pR – p)] (8.3) Acompressiblefluidisoneinwhichthevolumehasastrongdependenceonpressure.All gasesareinthiscategory.InChapter2,therealgaslawwasusedtodescribehowgasvolumesvary withpressure: V= znR ′T p (2.8) 8.3 The Classification of Reservoir Flow Systems 233 Unlikethecaseoftheslightlycompressiblefluids,thegasisothermalcompressibility,cg,cannotbe treatedasaconstantwithvaryingpressure.Infact,thefollowingexpressionforcgwasdeveloped: cg = 1 1 dz − p z dp (2.18) Althoughfluidsaretypedmainlybytheircompressibilities,inaddition,theremaybesinglephase ormultiphaseflow.Manysystemsareonlygas,oil,orwater,andmostoftheremainderareeither gas-oiloroil-watersystems.Forthepurposesofthischapter,discussionisrestrictedtocaseswhere thereisonlyasinglephaseflowing. Thetwogeometriesofgreatestpracticalinterestarethosethatgiverisetolinear and radial flow.Inlinearflow,asshowninFig.8.2,theflowlinesareparallelandthecrosssectionexposedto flowisconstant.Inradialflow,theflowlinesarestraightandconvergeintwodimensionstowarda commoncenter(i.e.,awellorcylinder).Thecrosssectionexposedtoflowdecreasesasthecenter isapproached.Occasionally,sphericalflowisofinterest,inwhichtheflowlinesarestraightand convergetowardacommoncenter(point)inthreedimensions.Althoughtheactualpathsofthe fluidparticlesinrocksareirregularduetotheshapeoftheporespaces,theoveralloraveragepaths mayberepresentedasstraightlinesinlinear,radial,orsphericalflow. Actually,noneofthesegeometriesisfoundpreciselyinpetroleumreservoirs,butformany engineeringpurposes,theactualgeometrymayoftenbecloselyrepresentedbyoneoftheseidealizations.Insometypesofreservoirstudies(i.e.,waterfloodingandgascycling),theseidealizations areinadequate,andmoresophisticatedmodelsarecommonlyusedintheirstead. Flowsystemsinreservoirrocksareclassified,accordingtotheirtimedependence,assteady state,transient,latetransient,orpseudosteadystate.Duringthelifeofawellorreservoir,thetype ofsystemcanchangeseveraltimes,whichsuggeststhatitiscriticaltoknowasmuchabouttheflow systemaspossibleinordertousetheappropriatemodeltodescribetherelationshipbetweenthe pressureandtheflowrate.Insteady-statesystems,thepressureandfluidsaturationsateverypoint throughoutthesystemdonotchange.Anapproximationtothesteady-stateconditionoccurswhen anyproductionfromareservoirisreplacedwithanequalmassoffluidfromsomeexternalsource. Linear Figure 8.2 Common flow geometries. Radial Spherical Chapter 8 234 • Single-Phase Fluid Flow in Reservoirs InChapter9,acaseofwaterinfluxisconsideredthatcomesclosetomeetingthisrequirement,but ingeneral,thereareveryfewsystemsthatcanbeassumedtohavesteady-stateconditions. Toconsidertheremainingthreeclassificationsoftimedependence,changesinpressureare discussedthatoccurwhenastepchangeintheflowrateofawelllocatedinthecenterofareservoir, asillustratedinFig.8.3,causesapressuredisturbanceinthereservoir.Thediscussionassumesthe following:(1)theflowsystemismadeupofareservoirofconstantthicknessandrockproperties, (2)theradiusofthecircularreservoirisre,and(3)theflowrateisconstantbeforeandaftertherate change.Astheflowrateischangedatthewell,themovementofpressurebeginstooccurawayfrom thewell.Themovementofpressureisadiffusionphenomenonandismodeledbythediffusivity equation(seesection8.5).Thepressuremovesatarateproportionaltotheformationdiffusivity,η, η= k φμ ct (8.4) wherekistheeffectivepermeabilityoftheflowingphase,φisthetotaleffectiveporosity,μisthe fluidviscosityoftheflowingphase,andctisthetotalcompressibility.Thetotalcompressibilityis obtainedbyweightingthecompressibilityofeachphasebyitssaturationandaddingtheformation compressibility,or pe Bound ary re rw pw h Figure 8.3 Schematic of a single well in a circular reservoir. 8.3 The Classification of Reservoir Flow Systems ct = cgSg + coSo + cwSw + cf 235 (8.5) Theformationcompressibility,cf ,shouldbeexpressedasthechangeinporevolumeperunitpore volumeperpsi.Duringthetimethepressureistravelingatthisrate,theflowstateissaidtobe transient.Whilethepressureisinthistransientregion,theouterboundaryofthereservoirhasno influenceonthepressuremovement,andthereservoiractsasifitwereinfiniteinsize. Thelatetransientregionistheperiodafterthepressurehasreachedtheouterboundaryofthe reservoirandbeforethepressurebehaviorhashadtimetostabilizeinthereservoir.Inthisregion, thepressurenolongertravelsatarateproportionaltoη.Itisverydifficulttodescribethepressure behaviorduringthisperiod. Thefourthperiod,thepseudosteadystate,istheperiodafterthepressurebehaviorhasstabilizedinthereservoir.Duringthisperiod,thepressureateverypointthroughoutthereservoiris changingataconstantrateandasalinearfunctionoftime.Thisperiodisoftenincorrectlyreferred toasthesteady-stateperiod. AnestimationforthetimewhenaflowsystemofthetypeshowninFig.8.3reachespseudosteadystatecanbemadefromthefollowingequation: t pss = 1200 re2 1200φμ ct re2 = η k (8.6) wheretpssisthetimetoreachthepseudosteadystate,expressedinhours.3Forawellproducingan oilwithareservoirviscosityof1.5cpandatotalcompressibilityof15×10–6 psi–1,fromacircular reservoirof1000-ftradiuswithapermeabilityof100mdandatotaleffectiveporosityof20%: t pss = 1200(0.2 )(1.5 )(15 × 10 −6 )(1000 2 ) = 54 hr 100 Thismeansthatapproximately54hours,or2.25days,isrequiredfortheflowinthisreservoirto reachpseudosteady-stateconditionsafterawelllocatedinitscenterisopenedtofloworfollowing achangeinthewellflowrate.Italsomeansthatifthewellisshutin,itwilltakeapproximately thistimeforthepressuretoequalizethroughoutthedrainageareaofthewell,sothatthemeasured subsurfacepressureequalstheaveragedrainageareapressureofthewell. Thissamecriterionmaybeappliedapproximatelytogasreservoirsbutwithlesscertaintybecause thegasismorecompressible.Foragasviscosityof0.015cpandacompressibilityof400×10–6 psi–1, t pss = 1200(0.2 )(0.015 )( 400 × 10 −6 )(1000 2 ) = 14.4 hr 100 Thus, under somewhat comparable conditions (i.e., the same re and k), gas reservoirs reach pseudosteady-stateconditionsmorerapidlythanoilreservoirs.Thisisduetothemuchlower viscosityofgases,whichmorethanoffsetstheincreaseinfluidcompressibility.Ontheother Chapter 8 236 • Single-Phase Fluid Flow in Reservoirs hand,gaswellsareusuallydrilledonwiderspacingssothatthevalueofre generally is larger forgaswellsthanforoilwells,thusincreasingthetimerequiredtoreachthepseudosteadystate. Manygasreservoirs,suchasthosefoundintheoverthrustbelt,aresandsoflowpermeability. Using an revalueof2500ftandapermeabilityof1md,whichwouldrepresentatightgassand, thenthefollowingvaluefortpss iscalculated: t pss = 1200(0.2 )(0.015 )( 400 × 10 −6 )(2500 2 ) = 9000 hr >1year 1 Thecalculationssuggestthatreachingpseudosteady-stateconditionsinatypicaltightgasreservoir takesaverylongtimecomparedtoatypicaloilreservoir.Ingeneral,pseudosteady-statemechanics sufficewhenthetimerequiredtoreachpseudosteadystateisshortcomparedwiththetimebetween substantialchangesintheflowrateor,inthecaseofreservoirs,withthetotalproducinglifeofthe reservoir.Manywellsarenotproducedataconstantrate,andinstead,theflowingpressuremay beapproximatelyconstant.Forsuchwellsduringthetransientflowcondition,thepressuredisturbancestillmovesatthesamevelocity,andatthetimeofpseudosteadystate,thewellreachesa boundary-dominatedcondition. 8.4 Steady-State Flow NowthatDarcy’slawhasbeenreviewedandtheclassificationofflowsystemshasbeendiscussed, the actual models that relate flow rate to reservoir pressure can be developed.The next several sectionscontainadiscussionofthesteady-statemodels.Bothlinearandradialflowgeometries arediscussedsincetherearemanyapplicationsforthesetypesofsystems.Forboththelinearand radialgeometries,equationsaredevelopedforallthreegeneraltypesoffluids(i.e.,incompressible, slightlycompressible,andcompressible). 8.4.1 Linear Flow of Incompressible Fluids, Steady State Figure8.4representslinearflowthroughabodyofconstantcrosssection,wherebothendsare entirelyopentoflowandwherenoflowcrossesthesides,top,orbottom.Ifthefluidisincompressible,oressentiallysoforallengineeringpurposes,thenthevelocityisthesameatallpoints,asis thetotalflowrateacrossanycrosssection;thus,inhorizontalflow, υ= qB k dp = −0.001127 μ dx Ac Separatingvariablesandintegratingoverthelengthoftheporousbody, qB L k dx = −0.001127 Ac ∫o μ p2 ∫p 1 dp 8.4 Steady-State Flow 237 P P1 P2 dP Q A dx x O Figure 8.4 L Representation of linear flow through a body of constant cross section. q = 0.001127 kAc ( p1 − p2 ) Bμ L (8.7) Forexample,underapressuredifferentialof100psiforapermeabilityof250md,afluidviscosity of2.5cp,aformationvolumefactorof1.127bbl/STB,alengthof450ft,andacross-sectionalarea of45sqft,theflowrateis q = 0.001127 (250 )( 45 )(100 ) = 1.0 STB/day (1.127 )(2.5 )( 450 ) Inthisintegration,B, q, μ, and kwereremovedfromtheintegralsign,assumingtheywereinvariant withpressure.Actually,forflowabovethebubblepoint,thevolume,andhencetherateofflow, varieswiththepressure,asexpressedbyEq.(8.2).Theformationvolumefactorandviscosityalso varywithpressure,asexplainedinChapter2.FattandDavishaveshownavariationinpermeabilitywithnetoverburdenpressureforseveralsandstones.4Thenetoverburdenpressureisthegross lesstheinternalfluidpressure;therefore,avariationofpermeabilitywithpressureisindicated, particularlyintheshallowerreservoirs.Becausetheseeffectsarenegligibleforafewhundred-psi pressuredifference,valuesattheaveragepressuremaybeusedformostpurposes. 8.4.2 Linear Flow of Slightly Compressible Fluids, Steady State Theequationforflowofslightlycompressiblefluidsismodifiedfromwhatwasjustderivedintheprevioussection,sincethevolumeofslightlycompressiblefluidsincreasesaspressuredecreases.Earlier Chapter 8 238 • Single-Phase Fluid Flow in Reservoirs inthischapter,Eq.(8.3)wasderived,whichdescribestherelationshipbetweenpressureandvolume foraslightlycompressiblefluid.Theproductoftheflowrate,definedinSTBunits,andtheformation volumefactorhavesimilardependenciesonpressure.Theproductoftheflowrateisgivenby qB = qR [1 + c(pR – p)] (8.8) whereqRistheflowrateatsomereferencepressure,pR.IfDarcy’slawiswrittenforthiscase,with variablesseparatedandtheresultingequationintegratedoverthelengthoftheporousbody,then thefollowingisobtained: qR Ac L k p2 ∫0 dx = −0.001127 μ ∫ p qR = − 1 dp 1 + c( p R − p ) 0.001127 kAc 1 + c( pR − p2 ) ln μ Lc 1 + c( pR − p1 ) (8.9) Thisintegrationassumesaconstantcompressibilityovertheentirepressuredrop.Forexample, underapressuredifferentialof100psiforapermeabilityof250md,afluidviscosityof2.5cp,a lengthof450ft,across-sectionalareaof45sqft,andaconstantcompressibilityof65(10–6)psi–1, choosingp1asthereferencepressure,theflowrateis q1 = (0.001127 )(250 )( 45 ) 1 + 65 × 10 −6 (100 ) 1n = 1.123 bbl/day 1 (2.5 )( 450 )(65 × 10 −6 ) Whencomparedwiththeflowratecalculationintheprecedingsection,q1isfoundtobedifferent duetotheassumptionofaslightlycompressiblefluidinthecalculationratherthananincompressiblefluid.NotealsothattheflowrateisnotinSTBunitsbecausethecalculationisbeingdoneata referencepressurethatisnotthestandardpressure.Ifp2ischosentobethereferencepressure,then theresultofthecalculationwillbeq2,andthevalueofthecalculatedflowratewillbedifferentstill becauseofthevolumedependenceonthereferencepressure: q2 = (0.001127 )(250 )( 45 ) 1 ln = 1.131 bbl/day −6 −6 (2.5 )( 450 )(65 × 10 ) 1 + 65 × 10 ( −100 ) Thecalculationsshowthatq1 and q2arenotlargelydifferent,whichconfirmswhatwasdiscussed earlier:thefactthatvolumeisnotastrongfunctionofpressureforslightlycompressiblefluids. 8.4.3 Linear Flow of Compressible Fluids, Steady State Therateofflowofgasexpressedinstandardcubicfeetperdayisthesameatallcrosssectionsin asteady-state,linearsystem.However,becausethegasexpandsasthepressuredrops,thevelocity 8.4 Steady-State Flow 239 isgreateratthedownstreamendthanattheupstreamend,andconsequently,thepressuregradient increasestowardthedownstreamend.TheflowatanycrosssectionxofFig.8.4wherethepressureispmaybeexpressedintermsoftheflowinstandardcubicfeetperdaybysubstitutingthe definitionofthegasformationvolumefactor: qBg = qpscTz 5.615Tsc p SubstitutinginDarcy’slaw, qpscTz k dp = −0.001127 5.615Tsc pAc μ dx Separatingvariablesandintegrating, qpscTz μ (5.615 )(0.001127 )kTsc Ac L p2 ∫0 dx = − ∫ p 1 p dp = 1 2 ( p1 − p22 ) 2 Finally, q= 0.003164Tsc Ac k ( p12 − p22 ) pscTzL μ (8.10) Forexample,whereTsc=60°F,Ac=45ft2, k=125md,p1=1000psia,p2 =500psia,psc=14.7psia, T=140°F,z=0.92,L=450ft,andμ =0.015cp, q= 0.003164 (520 )( 45 )(125 )(1000 2 − 500 2 ) = 126.7 MSCF/day 14.7(600 )(0.92 )( 450 )(0.015 ) Hereagain,T, k,andtheproduct μzwerewithdrawnfromtheintegralsasiftheywereinvariant withpressure,andasbefore,averagevaluesmaybeusedinthiscase.Atthispoint,itisinstructive toexamineanobservationthatWattenbargerandRameymadeaboutthebehaviorofthegasdeviationfactor—viscosityproductasafunctionofpressure.5Figure8.5isatypicalplotofμzversus pressureforarealgas.Notethattheproduct, μz,isnearlyconstantforpressureslessthanabout 2000psia.Above2000psia,theproduct μz/pisnearlyconstant.Althoughtheshapeofthecurve variesslightlyfordifferentgasesatdifferenttemperatures,thepressuredependenceisrepresentativeofmostnaturalgasesofinterest.Thepressureatwhichthecurvebendsvariesfromabout 1500psiato2000psiaforvariousgases.ThisvariationsuggeststhatEq.(8.10)isvalidonlyfor pressureslessthanabout1500psiato2000psia,dependingonthepropertiesoftheflowinggas. Chapter 8 • Single-Phase Fluid Flow in Reservoirs µz, cp 240 0 0 2000 4000 6000 8000 10,000 Pressure, p, psia Figure 8.5 Isothermal variation of μz with pressure. Abovethispressurerange,itwouldbemoreaccuratetoassumethattheproductμz/pisconstant. Forthecaseofμz/pconstant,thefollowingisobtained: qpscT ( z μ / p ) (5.615)(0.001127)kTsc Ac q= L p2 ∫0 dx = − ∫ p 1 dp = p1 − p2 0.006328 kTsc Ac ( p1 − p2 ) pscT ( z μ / p ) (8.11) InapplyingEq.(8.11),theproductμz/pshouldbeevaluatedattheaveragepressurebetweenp1 and p2. Al-Hussainy,Ramey,andCrawford,andRussel,Goodrich,Perry,andBruskotterintroduced atransformationofvariablesthatleadstoanothersolutionforgasflowinthesteady-stateregion.6,7 Thetransformationinvolvestherealgaspseudopressure,m(p),whichhasunitsofpsia2/cpinstandardfieldunitsandisdefinedas 8.4 Steady-State Flow 241 m( p ) = 2 ∫ p pR p dp μz (8.12) wherepRisareferencepressure,usuallychosentobe14.7psia,fromwhichthefunctionisevaluated. Usingtherealgaspseudopressure,theequationforgasflowingundersteady-stateconditionsbecomes q= 0.003164Tsc Ac k ( m( p1 ) − m( p2 )) pscTL (8.13) TheuseofEq.(8.13)requiresvaluesoftherealgaspseudopressure.Theprocedureused tofindvaluesofm(p)hasbeendiscussedintheliterature.8,9Theprocedureinvolvesdetermining μ and zforseveralpressuresoverthepressurerangeofinterest,usingthemethodsofChapter2. Valuesofp/μzarethencalculated,andaplotofp/μzversuspismade,asillustratedinFig.8.6.A numericalintegrationschemesuchasSimpson’sruleisthenusedtodeterminethevalueofthearea fromthereferencepressureuptoapressureofinterest,p1.Thevalueofm(p1)thatcorresponds withpressure,p1,isgivenby m(p1)=2(area1) where area1 = p1 ∫p R p dp μz Therealgaspseudopressuremethodcanbeappliedatanypressureofinterestifthedataareavailable. p µ2 Area pr Figure 8.6 Graphical determination of m(p). p1 p Chapter 8 242 P1 Q Figure 8.7 8.4.4 • Single-Phase Fluid Flow in Reservoirs P4 P3 P2 AC K1 K2 K3 L1 L2 L3 Series flow in linear beds. Permeability Averaging in Linear Systems Consider two or more beds of equal cross section but of unequal lengths and permeabilities (Fig.8.7,depictingflowinseries)inwhichthesamelinearflowrateqexists,assuminganincompressiblefluid.Obviouslythepressuredropsareadditive,and (p1 – p4)=(p1 – p2)+(p2 – p3)+(p3 – p4) SubstitutingtheequivalentsofthesepressuredropsfromEq.(8.7), qt Bμ Lt q1 Bμ L1 q2 Bμ L2 q3 B μ L 3 + = + 0.001127 kavg Ac 0.001127 k1 Ac1 0.001127 k2 Ac 2 0.001127 k3 Ac 3 Butsincetheflowrates,crosssections,viscosities,andformationvolumefactors(neglectingthe changewithpressure)areequalinallbeds, Lt L L L = 1+ 2+ 3 kavg k1 k2 k3 or kavg = Lt ∑ Li = L1 L2 L3 ∑ Li / ki + + k1 k2 k3 (8.14) 8.4 Steady-State Flow 243 TheaveragepermeabilityasdefinedbyEq.(8.14)isthatpermeabilitytowhichanumberofbeds ofvariousgeometriesandpermeabilitiescouldbeapproximatedbyandyieldthesametotalflow rateunderthesameappliedpressuredrop. Equation (8.14) was derived using the incompressible fluid equation. Because the permeabilityisapropertyoftherockandnotofthefluidsflowingthroughit,exceptforgasesatlow pressure,theaveragepermeabilitymustbeequallyapplicabletogases.Thisrequirementmaybe demonstratedbyobservingthat,forpressuresbelow1500psiato2000psia, ( p12 − p42 ) = ( p12 − p22 ) + ( p22 − p32 ) + ( p32 − p42 ) SubstitutingtheequivalentsfromEq.(8.10),thesameEq.(8.14)isobtained. Theaveragepermeabilityof10md,50md,and1000mdbeds(whichare6ft,18ft,and40 ftinlength,respectively,butofequalcrosssection)whenplacedinseriesis kavg = ∑ Li 6 + 18 + 40 = = 64 md ∑ Li / ki 6 / 10 + 18 / 50 + 40 / 1000 Consider two or more beds of equal length but unequal cross sections and permeabilities flowingthesamefluidinlinearflowunderthesamepressuredrop(p1top2),asshowninFig.8.8, depictingparallelflow.Obviouslythetotalflowisthesumoftheindividualflows,or qt = q1 + q2 + q3 P1 Q1 Q2 P2 AC1 K1 AC2 K2 Q3 AC3 K3 L Figure 8.8 Parallel flow in linear beds. Chapter 8 244 • Single-Phase Fluid Flow in Reservoirs and kavg Act ( p1 − p2 ) B μL = k1 Ac1 ( p1 − p2 ) k2 Ac 2 ( p1 − p2 ) k3 Ac 3 ( p1 − p2 ) + + B μL B μL B μL canceling kavgAct = k1 Ac1 + k2Ac2 + k3Ac3 kavg = ∑ ki Aci ∑ Aci (8.15) Andwhereallbedsareofthesamewidth,sothattheirareasareproportionaltotheirthicknesses, kavg = ∑ ki hi ∑ hi (8.16) Wheretheparallelbedsarehomogeneousinpermeabilityandfluidcontent,thepressureandthe pressuregradientarethesameinallbedsatequaldistances.Thustherewillbenocrossflowbetweenbeds,owingtofluidpressuredifferences.However,whenwaterdisplacesoil—forexample fromasetofparallelbeds—theratesofadvanceofthefloodfrontswillbegreaterinthemore permeablebeds.Becausethemobilityoftheoil(ko/μo)aheadofthefloodfrontisdifferentfromthe mobilityofwater(kw/μw)behindthefloodfront,thepressuregradientswillbedifferent.Inthisinstance,therewillbepressuredifferencesbetweentwopointsatthesamedistancethroughtherock, andcrossflowwilltakeplacebetweenthebedsiftheyarenotseparatedbyimpermeablebarriers. Underthesecircumstances,Eqs.(8.15)and(8.16)arenotstrictlyapplicable,andtheaveragepermeabilitychangeswiththestageofdisplacement.Watermayalsomovefromthemorepermeable tothelesspermeablebedsbycapillaryaction,whichfurthercomplicatesthestudyofparallelflow. Theaveragepermeabilityofthreebedsof10md,50md,and1000mdand6ft,18ft,and 36ft,respectively,inthicknessbutofequalwidth,whenplacedinparallelis kavg = 8.4.5 ∑ ki hi 10 × 6 + 18 × 50 + 36 × 1000 = = 616md ∑ hi 6 + 18 + 36 Flow through Capillaries and Fractures Althoughtheporespaceswithinrocksseldomresemblestraight,smooth-walledcapillarytubesof constantdiameter,itisoftenconvenientandinstructivetotreattheseporespacesasiftheywere composedofbundlesofparallelcapillarytubesofvariousdiameters.Consideracapillarytubeof lengthLandinsideradiusro,whichisflowinganincompressiblefluidofμviscosityinlaminaror 8.4 Steady-State Flow 245 viscousflowunderapressuredifferenceof(p1 – p2).Fromfluiddynamics,Poiseuille’slaw,which describesthetotalflowratethroughthecapillary,canbewrittenas q = 1.30(10 )10 π ro4 ( p1 − p2 ) Bμ L (8.17) Darcy’s law for the linear flow of incompressible fluids in permeable beds, Eq. (8.7), and Poiseuille’slawforincompressiblefluidcapillaryflow,Eq.(8.15),arequitesimilar: q = 0.001127 kAc ( p1 − p2 ) B μL (8.7) WritingAc = π r02 forareainEq.(8.7)andequatingittoEq.(8.17), k=1.15(10)13 r02 (8.18) Thusthepermeabilityofarockcomposedofcloselypackedcapillaries,eachhavingaradiusof 4.17(10)–6ft(0.00005in.),isabout200md.Andifonly25%oftherockconsistsofporechannels (i.e.,ithas25%porosity),thepermeabilityisaboutone-fourthaslarge,orabout50md. Anequationfortheviscousflowofincompressiblewettingfluidsthroughsmoothfractures ofconstantwidthmaybeobtainedas q = 8.7(10 )9 W 2 Ac ( p1 − p2 ) Bμ L (8.19) InEq.(8.19),Wisthewidthofthefracture;Acisthecross-sectionalareaofthefracture,which equalstheproductofthewidthWandlateralextentofthefracture;andthepressuredifferenceis thatwhichexistsbetweentheendsofthefractureoflengthL.Equation(8.19)maybecombined withEq.(8.7)toobtainanexpressionforthepermeabilityofafractureas k=7.7(10)12W2 (8.20) Thepermeabilityofafractureonly8.33(10)–5ftwide(0.001in.)is53,500md. Fracturesandsolutionchannelsaccountforeconomicproductionratesinmanydolomite, limestone,andsandstonerocks,whichcouldnotbeproducedeconomicallyifsuchopeningsdid notexist.Consider,forexample,arockofverylowprimaryormatrixpermeability,say0.01md, thatcontainsontheaverageafracture4.17(10)–4ftwideand1ftinlateralextentpersquarefoot ofrock.Assumingthefractureisinthedirectioninwhichflowisdesired,thelawofparallelflow, Eq.(8.15),willapply,and Chapter 8 246 kavg = • Single-Phase Fluid Flow in Reservoirs 0.01[1 − (1)( 4.17(10 )−4 )] + ( 7.7(10 )12 ( 4.17(10 )−4 )2 [1( 4.17(10 )−4 )] 1 kavg=558md 8.4.6 Radial Flow of Incompressible Fluids, Steady State Consider radial flow toward a vertical wellbore of radius rw in a horizontal stratum of uniform thicknessandpermeability,asshowninFig.8.9.Ifthefluidisincompressible,theflowacrossany circumferenceisaconstant.Letpwbethepressuremaintainedinthewellborewhenthewellis flowingqSTB/dayandapressurepeismaintainedattheexternalradiusre.Letthepressureatany radiusrbep.Thenatthisradiusr, qB qB k dp = = −0.001127 Ac 2π rh μ dr υ= wherepositiveqisinthepositiverdirection.Separatingvariablesandintegratingbetweenanytwo radii, r1 and r2,wherethepressuresarep1 and p2,respectively, r2 ∫r 1 p2 k qB dr = −0.001127 ∫ dp p 1 μ 2π rh q=− 0.00708 kh ( p2 − p1 ) μ B ln (r2 / r1 ) Theminussignisusuallydispensedwith,forwherep2isgreaterthanp1,theflowisknowntobe negative—thatis,inthenegativerdirection,ortowardthewellbore: re pw r p pe rw H Figure 8.9 Representation of radial flow toward a vertical well. 8.4 Steady-State Flow 247 q= 0.00708 kh ( p2 − p1 ) μ B ln (r2 / r1 ) Frequentlythetworadiiofinterestarethewellboreradiusrwandtheexternalordrainageradius re.Then q= 0.00708 kh ( pe − pw ) μ B ln (re / rw ) (8.21) Theexternalradiusisusuallyinferredfromthewellspacing.Forexample,acircleof660ftradius canbeinscribedwithinasquare40acunit,so660ftiscommonlyusedforrewith40acspacing. Sometimesaradiusof745ftisused,thisbeingtheradiusofacircle40acinarea.Thewellbore radiusisusuallyassignedfromthebitdiameter,thecasingdiameter,oracalipersurvey.Inpractice, neithertheexternalradiusnorthewellboreradiusisgenerallyknownwithprecision.Fortunately, theyentertheequationasalogarithm,sothattheerrorintheequationwillbemuchlessthanthe errorsintheradii.Sincewellboreradiiareabout1/3ftand40acspacing(rc=660ft)isquitecommon,aratio2000isquitecommonlyusedforre/rw.Sinceln2000is7.60andln3000is8.00,a50% increaseinthevalueofre/rwgivesonlya5.3%increaseinthevalueofthelogarithm. TheexternalpressurepeusedinEq.(8.21)isgenerallytakenasthestaticwellpressurecorrectedtothemiddleoftheproducinginterval,andtheflowingwellpressurepwistheflowingwell pressurealsocorrectedtothemiddleoftheproducingintervalduringaperiodofstabilizedflow atrateq.Whenreservoirpressurestabilizesasundernaturalwaterdriveorpressuremaintenance, Eq.(8.21)isquiteapplicablebecausethepressureismaintainedattheexternalboundary,andthe fluidproducedatthewellisreplacedbyfluidcrossingtheexternalboundary.Theflow,however, maynotbestrictlyradial. 8.4.7 Radial Flow of Slightly Compressible Fluids, Steady State Equation(8.3)isagainusedtoexpressthevolumedependenceonpressureforslightlycompressible fluids. If this equation is substituted into the radial form of Darcy’s law, the following is obtained: qB = qR [1 + c( pR − p )] k dp = −0.001127 2π rh μ dr Separatingthevariables,assumingaconstantcompressibilityovertheentirepressuredrop,and integratingoverthelengthoftheporousmedium, qR = 0.00708 kh 1 + c( pR − p2 ) ln μ c ln (r2 /r1 ) 1 + c( pR − p1 ) (8.22) Chapter 8 248 8.4.8 • Single-Phase Fluid Flow in Reservoirs Radial Flow of Compressible Fluids, Steady State TheflowofagasatanyradiusrofFig.8.8,wherethepressureisp,maybeexpressedintermsof theflowinstandardcubicfeetperdayby qBg = qpscTz 5.615Tsc p SubstitutingintheradialformofDarcy’slaw, qpscTz k dp = −0.001127 5.615Tsc p(2π rh ) μ dr Separatingvariablesandintegrating, r2 dr p2 qpscTz μ 1 = − ∫ p dp = ( p12 − p22 ) ∫ p1 5.615(0.001127 )(2π )Tsc kh r1 r 2 or Finally, qpscTz μ ln(r2 / r1 ) = p12 − p22 0.01988Tsc kh q= 0.01988Tsc kh( p12 − p22 ) pscT ( z μ )ln (r2 / r1 ) (8.23) TheproductμzhasbeenassumedtobeconstantforthederivationofEq.(8.23).Itwaspointedout insection8.4.3thatthisisusuallytrueonlyforpressureslessthanabout1500psiato2000psia. Forgreaterpressures,itwasstatedthatabetterassumptionwasthattheproductμz/pwasconstant. Forthiscase,thefollowingisobtained: q= 0.03976Tsc kh ( p1 − p2 ) pscT ( z μ / p )ln (r2 / r1 ) (8.24) Applying Eqs. (8.23) and (8.24), the products μz and μz/p should be calculated at the average pressurebetweenp1 and p2. Iftherealgaspseudopressurefunctionisused,theequationbecomes q= 0.01988Tsc kh( m( p1 ) − m( p2 )) pscTln (r2 / r1 ) (8.25) 8.4 Steady-State Flow 8.4.9 249 Permeability Averages for Radial Flow Manyproducingformationsarecomposedofstrataorstringersthatmayvarywidelyinpermeabilityandthickness,asillustratedinFig.8.10.Ifthesestrataareproducingfluidtoacommonwellbore underthesamedrawdownandfromthesamedrainageradius,then qt = q1 + q2 + q3+…+qn 0.00708 kavg ht ( pe − pw ) μ B ln (re / rw ) = 0.00708 k1h1 ( pe − pw ) 0.00708 k2 h2 ( pe − pw ) + etc. + μ B ln (re / rw ) μ B ln (re / rw ) Then,canceling, kavght = k1h1 + k2h2 +…+knhn kavg = ∑ ki hi ∑ hi (8.26) Thisequationisthesameasforparallelflowinlinearbedswiththesamebedwidth.Here,again, averagepermeabilityreferstothatpermeabilitybywhichallbedscouldbereplacedandstillobtain thesameproductionrateunderthesamedrawdown.Theproductkhiscalledtheflowcapacity or transmissivityofabedorstratum,andthetotal flow capacityoftheproducingformation,Σkihi, is usuallyexpressedinmillidarcy-feet.Becausetherateofflowisdirectlyproportionaltotheflow capacity,Eq.(8.21),a10-ftbedof100mdwillhavethesameproductionrateasa100-ftbedof 10-mdpermeability,otherthingsbeingequal.Therearelimitsofformationflowcapacitybelow qt Figure 8.10 Radial flow in parallel beds. q1 h1 k1 q2 h2 k2 q3 h3 k3 Chapter 8 250 • Single-Phase Fluid Flow in Reservoirs whichproductionratesarenoteconomic,justastherearelimitsofnetproductiveformationthicknessesbelowwhichwellswillneverpayout.Oftwoformationswiththesameflowcapacity,the onewiththeloweroilviscositymaybeeconomicbuttheothermaynot,andtheavailablepressuredrawdownentersinsimilarly.Netsandthicknessesoftheorderof5ftandcapacitiesofthe orderofafewhundredmillidarcy-feetarelikelytobeuneconomic,dependingonotherfactors suchasavailabledrawdown,viscosity,porosity,connatewater,depth,andthelike,orwillrequire hydraulicfracturestimulation.Theflowcapacityoftheformationtogetherwiththeviscosityalso determinestoalargeextentwhetherawellwillfloworwhetherartificialliftmustbeused.The amountofsolutiongasisanimportantfactor.Withhydraulicfracturing(tobediscussedlater),the wellproductivityinlowflowcapacityreservoirscanbegreatlyimproved. Wenowconsideraradialflowsystemofconstantthicknesswithapermeabilityofkebetween thedrainageradiusreandsomelesserradiusra and an alteredpermeabilitykabetweentheradiusra andthewellboreradiusrw,asshowninFig.8.11.Thepressuredropsareadditive,and (pe – pw)=(pe – pa)+(pa – pw) Then,fromEq.(8.21), q μ B ln (re / rw ) q μ B ln (re / ra ) q μ B ln (ra / rw ) + = 0.00708 kavg h 0.00708 ke h 0.00708 ka h Cancelingandsolvingforkavg, kavg = rw pw ka ke ln (re / rw ) ka ln (re / ra ) + ke ln (ra / rw ) ra Figure 8.11 re pa ka Radial flow in beds in series. (8.27) pe ke 8.5 Development of the Radial Diffusivity Equation 251 Equation(8.27)maybeextendedtoincludethreeormorezonesinseries.Thisequationisimportantinstudyingtheeffectofadecreaseorincreaseofpermeabilityinthezoneaboutthewellbore onthewellproductivity. 8.5 Development of the Radial Diffusivity Equation Theradialdiffusivityequation,whichisthegeneraldifferentialequationusedtomodeltime-dependentflowsystems,isnowdeveloped.ConsiderthevolumeelementshowninFig.8.12.The elementhasathicknessΔrandislocatedrdistancefromthecenterofthewell.Massisallowed toflowintoandoutofthevolumeelementduringaperiodΔt.Thevolumeelementisinareservoirofconstantthicknessandconstantproperties.Flowisallowedinonlytheradialdirection. Thefollowingnomenclature,whichisthesamenomenclaturedefinedpreviously,isused: q=volumeflowrate,STB/dayforincompressibleandslightlycompressiblefluidsand SCF/dayforcompressiblefluids ρ=densityofflowingfluidatreservoirconditions,lb/ft3 r=distancefromwellbore,ft h=formationthickness,ft υ=velocityofflowingfluid,bbl/day-ft2 t=hours φ=porosity,fraction k=permeability,md μ=flowingfluidviscosity,cp Withtheseassumptionsanddefinitions,amassbalancecanbewrittenaroundthevolumeelement overthetimeintervalΔt.Inwordform,themassbalanceiswrittenas (qρ )r + ∆r (qρ )r h r r + ∆r Figure 8.12 Volume element used in the development of the radial differential equation. 252 Chapter 8 • Single-Phase Fluid Flow in Reservoirs MassenteringvolumeelementduringintervalΔt–Massleavingvolumeelement duringintervalΔt =ChangeofmassinvolumeelementduringintervalΔt ThemassenteringthevolumeelementduringΔtisgivenby (qBρΔt )r + Δ r = 2π (r + Δ r)h( ρυ (5.615 / 24 )Δ t)r + Δr (8.28) ThemassleavingthevolumeelementduringΔtisgivenby (qBρΔt)r=2πrh(ρυ(5.615/24)Δt)r (8.29) ThechangeofmassintheelementduringtheintervalΔtisgivenby 2π r Δrh[(φρ )t + Δt − (φρ )t ] (8.30) CombiningEqs.(8.28),(8.29),and(8.30),assuggestedbytheword“equation”writtenabove, 2π (r + r )h( ρυ (5.615 / 24 )Δt )r + Δr − 2π rh( ρυ (5.615 / 24 )Δt )r = 2π r Δrh[(φρ )t + Δt − (φρ )t ] Ifbothsidesofthisequationaredividedby2πrΔrhΔtandthelimitistakenineachtermasΔr and Δtapproachzero,thefollowingisobtained: 1 ∂ ∂ (0.234 ρυ ) + (0.234 ρυ ) = (φρ ) ∂r r ∂t or 0.234 ∂ ∂ (r ρυ ) = (φρ ) r ∂r ∂t (8.31) Equation(8.31)isthecontinuityequationandisvalidforanyflowsystemofradialgeometry.To obtaintheradialdifferentialequationthatwillbethebasisfortime-dependentmodels,pressure mustbeintroducedandφeliminatedfromthepartialderivativetermontheright-handsideofEq. (8.31).Todothis,Darcy’sequationmustbeintroducedtorelatethefluidflowratetoreservoir pressure: υ = −0.001127 k ∂p μ ∂r 8.6 Transient Flow 253 RealizingthattheminussigncanbedroppedfromDarcy’sequationbecauseofthesignconvention forfluidflowinporousmediaandsubstitutingDarcy’sequationintoEq.(8.31), 0.234 ∂ k ∂p ∂ 0.001127 ρr = (φρ ) r ∂r μ ∂r ∂t (8.32) Theporosityfromthepartialderivativetermontheright-handsideiseliminatedbyexpandingthe right-handsideandtakingtheindicatedderivatives: ∂ ∂ρ ∂φ (φρ ) = φ +ρ ∂t ∂t ∂t (8.33) Itcanbeshownthatporosityisrelatedtotheformationcompressibilitybythefollowing: cf = 1 ∂φ φ ∂p (8.34) Applyingthechainruleofdifferentiationto∂φ/∂t, ∂φ ∂φ ∂p = ∂t ∂p ∂t SubstitutingEq.(8.34)intothisequation, ∂φ ∂p = φc f ∂t ∂t Finally,substitutingthisequationintoEq.(8.33)andtheresultintoEq.(8.29), ∂p ∂ρ ∂p 0.234 ∂ k +φ 0.001127 ρr = ρϕ c f ∂t ∂t ∂r r ∂r μ (8.35) Equation(8.35)isthegeneralpartialdifferentialequationusedtodescribetheflowofanyfluid flowinginaradialdirectioninporousmedia.Inadditiontotheinitialassumptions,Darcy’sequationhasbeenadded,whichimpliesthattheflowislaminar.Otherwise,theequationisnotrestricted toanytypeoffluidoranyparticulartimeregion. 8.6 Transient Flow Byapplyingappropriateboundaryandinitialconditions,particularsolutionstothedifferentialequationderivedintheprecedingsectioncanbediscussed.Thesolutionsobtainedpertaintothetransient 254 Chapter 8 • Single-Phase Fluid Flow in Reservoirs andpseudosteady-stateflowperiodsforbothslightlycompressibleandcompressiblefluids.Sincethe incompressiblefluiddoesnotexist,solutionsinvolvingthistypeoffluidarenotdiscussed.Onlythe radialflowgeometryisconsideredbecauseitisthemostusefulandapplicablegeometry.Ifthereader isinterestedinlinearflow,MatthewsandRussellpresentthenecessaryequations.10Also,duetothe complexnatureofthepressurebehaviorduringthelate-transientperiod,solutionsofthedifferential equationforthistimeregionarenotconsidered.Tofurtherjustifynotconsideringflowmodelsfrom thisperiod,itistruethatthemostpracticalapplicationsinvolvethetransientandpseudosteady-state periods. 8.6.1 Radial Flow of Slightly Compressible Fluids, Transient Flow IfEq.(8.2)isexpressedintermsofdensity, ρ,whichistheinverseofspecificvolume,thenthe followingisobtained: ρ = ρ R ec ( p − pR ) (8.36) wherepRissomereferencepressureandρRisthedensityatthatreferencepressure.Inherentin thisequationistheassumptionthatthecompressibilityofthefluidisconstant.Thisisnearly alwaysagoodassumptionoverthepressurerangeofagivenapplication.SubstitutingEq.(8.36) intoEq.(8.35), 0.234 ∂ k ∂p ∂p ∂ 0.001127 [ ρR ec ( p − pR ) ]r = [ ρR ec ( p − pR ) ]φ c f + φ [ ρ R ec ( p − pR ) ] r ∂r μ ∂r ∂t ∂t Tosimplifythisequation,onemustmaketheassumptionthatk and μareconstantoverthepressure,time,anddistancerangesinapplyingtheequation.Thisisrarelytrueaboutk.However,ifk isassumedtobeavolumetricaveragepermeabilityovertheseranges,thentheassumptionisgood. Inaddition,ithasbeenfoundthatviscositiesofliquidsdonotchangesignificantlyovertypical pressurerangesofinterest.Makingthisassumptionallowsk/μtobebroughtoutsidethederivative. Takingthenecessaryderivativesandsimplifying, 2 ∂2 p 1 ∂p ∂p φμ ∂p + + = (c f + c ) 2 ∂ ∂ r r . 0 002637 r k ∂t ∂r or 2 ∂p ∂2 p 1 ∂p ∂p φμ ct = + + 0.002637 k ∂t ∂r 2 r ∂r ∂r (8.37) Thelasttermontheleft-handsideofEq.(8.37)causesthisequationtobenonlinearandverydifficulttosolve.However,ithasbeenfoundthatthetermisverysmallformostapplicationsoffluid 8.6 Transient Flow 255 flowinvolvingliquids.Whenthistermbecomesnegligibleforthecaseofliquidflow,Eq.(8.37) reducesto ∂p ∂2 p 1 ∂p φμ ct + = 2 ∂ ∂t 0 002637 . r r k ∂r (8.38) Thisequationisthediffusivityequationinradialform.Thenamecomesfromitsapplicationtothe radialflowofthediffusionofheat.Basically,theflowofheat,flowofelectricity,andflowoffluids inpermeablerockscanbedescribedbythesamemathematicalforms.Thegroupofterms φμct/k waspreviouslydefinedtobeequalto1/η,where ηiscalledthediffusivityconstant(seesection 8.3).ThissameconstantwasencounteredinEq.(8.6)forthereadjustmenttime. ToobtainasolutiontoEq.(8.38),itisnecessaryfirsttospecifyoneinitialandtwoboundary conditions.Theinitialconditionissimplythatattimet=0,thereservoirpressureisequaltothe initialreservoirpressure,pi.ThefirstboundaryconditionisgivenbyDarcy’sequationifitisrequiredthattherebeaconstantrateatthewellbore: q = −0.001127 kh ∂p (2π r ) ∂r r = r Bμ w Thesecondboundaryconditionisgivenbythefactthatthedesiredsolutionisforthetransientperiod.Forthisperiod,thereservoirbehavesasifitwereinfiniteinsize.Thissuggeststhatatr = ∞, thereservoirpressurewillremainequaltotheinitialreservoirpressure,pi.Withtheseconditions, MatthewsandRusselgavethefollowingsolution: p(r, t ) = pi − 70.6 qμ B φμ ct r 2 − Ei − kh 0.00105 kt (8.39) whereallvariablesareconsistentwithunitsthathavebeendefinedpreviously—thatis,p(r, t)and pi are in psia, qisinSTB/day,μisincp,B(formationvolumefactor)isinbbl/STB,kisinmd,h is inft,ct is in psi–1, risinft,andtisinhr.10Equation(8.39)iscalledtheline source solutiontothe diffusivityequationandisusedtopredictthereservoirpressureasafunctionoftimeandposition. Themathematicalfunction,Ei,istheexponentialintegralandisdefinedby Ei ( − x ) = − ∫ x e− u du x x2 x3 − + etc. = 1n x − + ! ( !) ( !) 1 2 2 3 3 u ThisintegralhasbeencalculatedasafunctionofxandispresentedinTable8.1,fromwhichFig. 8.13wasdeveloped. 10.0 Exponential integral values 8.0 ∞ 6.0 Ei(–x) = – x 4.0 ∫ e–u du u For x < 0.02 Ei(–x) = ln(x) + 0.577 3.0 2.0 0 –.02 –.04 1.0 –.08 –.06 –.10 Ei(–x) 0.8 (x) 0.6 0.4 0.3 0.2 0.1 .08 .06 .04 .03 .02 .01 0 −0.5 −1.0 −1.5 −2.0 Ei(–x) Figure 8.13 Plot of exponential integral function. 256 −2.5 −3.0 −3.5 Table 8.1 Values of –Ei(–x) as a Function of x x –Ei (–x) x –Ei (–x) x –Ei (–x) 0.1 1.82292 4.3 0.00263 8.5 0.00002 0.2 1.22265 4.4 0.00234 8.6 0.00002 0.3 0.90568 4.5 0.00207 8.7 0.00002 0.4 0.70238 4.6 0.00184 8.8 0.00002 0.5 0.55977 4.7 0.00164 8.9 0.00001 0.6 0.45438 4.8 0.00145 9.0 0.00001 0.7 0.37377 4.9 0.00129 9.1 0.00001 0.8 0.31060 5.0 0.00115 9.2 0.00001 0.9 0.26018 5.1 0.00102 9.3 0.00001 1.0 0.21938 5.2 0.00091 9.4 0.00001 1.1 0.18599 5.3 0.00081 9.5 0.00001 1.2 0.15841 5.4 0.00072 9.6 0.00001 1.3 0.13545 5.5 0.00064 9.7 0.00001 1.4 0.11622 5.6 0.00057 9.8 0.00001 1.5 0.10002 5.7 0.00051 9.9 0.00000 1.6 0.08631 5.8 0.00045 10.0 0.00000 1.7 0.07465 5.9 0.00040 1.8 0.06471 6.0 0.00036 1.9 0.05620 6.1 0.00032 2.0 0.04890 6.2 0.00029 2.1 0.04261 6.3 0.00026 2.2 0.03719 6.4 0.00023 2.3 0.03250 6.5 0.00020 2.4 0.02844 6.6 0.00018 2.5 0.02491 6.7 0.00016 2.6 0.02185 6.8 0.00014 2.7 0.01918 6.9 0.00013 2.8 0.01686 7.0 0.00012 2.9 0.01482 7.1 0.00010 3.0 0.01305 7.2 0.00009 3.1 0.01149 7.3 0.00008 3.2 0.01013 7.4 0.00007 3.3 0.00894 7.5 0.00007 (continued) 257 Chapter 8 258 • Single-Phase Fluid Flow in Reservoirs Table 8.1 Values of –Ei(–x) as a Function of x (continued) x –Ei (–x) x –Ei (–x) 3.4 0.00789 7.6 0.00006 3.5 0.00697 7.7 0.00005 3.6 0.00616 7.8 0.00005 3.7 0.00545 7.9 0.00004 3.8 0.00482 8.0 0.00004 3.9 0.00427 8.1 0.00003 4.0 0.00378 8.2 0.00003 4.1 0.00335 8.3 0.00003 4.2 0.00297 8.4 0.00002 x –Ei (–x) Equation(8.39)canbeusedtofindthepressuredrop(pi – p)thatwillhaveoccurredatany radiusaboutaflowingwellafterthewellhasflowedatarate,q,forsometime,t.Forexample, considerareservoirwhereoilisflowingandμo=0.72cp,Bo=1.475bbl/STB,k=100md,h=15 ft,ct=15×10–6 psi–1, φ=23.4%,andpi=3000psia.Afterawellisproducedat200STB/dayfor 10days,thepressureataradiusof1000ftwillbe p = 3000 − 0.234 (0.72 )15(10 )−6 (1000 )2 70.6(200 )(0.72 )(1.475 ) − Ei − 100(15 ) 0.00105(100 )(10 )(24 ) Thus p=3000+10.0Ei(–0.10) FromFig.8.13,Ei(–0.10)=–1.82.Therefore, p=3000+10.0(–1.82)=2981.8psia Figure8.14showsthispressureplottedonthe10-daycurveandshowsthepressuredistributionsat 0.1,1.0,and100daysforthesameflowconditions. Ithasbeenshownthat,forvaluesoftheEifunctionargument,lessthan0.01thefollowing approximationcanbemade: – Ei(–x)=–ln(x)–0.5772 8.6 Transient Flow 259 3000 y Pressure, psia 2950 T .1 =0 T .0 =1 T= y da s ay T= 2900 da d 10 ys 0 10 da 2850 2800 1 10 100 Radius, ft 1000 10,000 Figure 8.14 Pressure distribution about a well at four time periods after start of production. Thissuggeststhat φμ ct r 2 < 0.01 0.00105 kt Byrearrangingtheequationandsolvingfort,thetimerequiredtomakethisapproximationvalid forthepressuredetermination1000ftfromtheproducingwellcanbefound: t> 0.234 (0.72 )15(10 )−6 (1000 )2 ≈ 2400hr = 100days 0.00105(100 )(0.01) TodetermineiftheapproximationtotheEifunctionisvalidwhencalculatingthepressureatthe sandfaceofaproducingwell,itisnecessarytoassumeawellboreradius,rw(0.25ft),andtocalculatethetimethatwouldmaketheapproximationvalid.Thefollowingisobtained: t> 0.234 (0.72 )15(10 )−6 (0.25 )2 ≈ 0.0002 hours 0.00105(100 )(0.01) Chapter 8 260 • Single-Phase Fluid Flow in Reservoirs Itisapparentfromthesecalculationsthatwhethertheapproximationcanbeusedisastrongfunctionofthedistancefromthepressuredisturbancetothepointatwhichthepressuredetermination isdesiredor,inthiscase,fromtheproducingwell.Forallpracticalpurposes,theassumptionis validwhenconsideringpressuresatthepointofthedisturbance.Therefore,atthewellboreand wherevertheassumptionisvalid,Eq.(8.39)canberewrittenas p(r, t ) = pi − 70.6 qμ B φμ ct r 2 − 0.5772 1n − kh 0.00105 kt Substitutingthelogbase10intothisequationforthelnterm,rearrangingandsimplifying,onegets p(r, t ) = pi − 162.6 qμ B kt − 3.23 log 2 kh φμ ct r (8.40) Equation(8.40)servesasthebasisforawelltestingprocedurecalledtransient well testing, a very usefultechniquethatisdiscussedlaterinthischapter. 8.6.2 Radial Flow of Compressible Fluids, Transient Flow Insection8.5,Eq.(8.35) ∂p ∂ρ ∂p 0.234 ∂ k +φ 0.001127 ρr = ρφ c f ∂t ∂t ∂r r ∂r μ (8.35) wasdevelopedtodescribetheflowofanyfluidflowinginaradialgeometryinporousmedia.To developasolutiontoEq.(8.35)forthecompressiblefluid,orgas,case,twoadditionalequations arerequired:(1)anequationofstate,usuallytherealgaslaw,whichisEq.(2.8),and(2)Eq.(2.18), whichdescribeshowthegasisothermalcompressibilityvarieswithpressure: pV = znR′T cg = 1 1 dz − p z dp (2.8) (2.18) Thesethreeequationscanbecombinedtoyield φ ct p 1 ∂ p ∂p ∂p r = r ∂r μ z ∂r 0.0002637 kz ∂t (8.41) 8.7 Pseudosteady-State Flow 261 ApplyingtherealgaspseudopressuretransformationtoEq.(8.41)yieldsthefollowing: ∂m( p ) ∂2 m( p ) 1 ∂m( p ) φμ ct + = r ∂r 0.0002637 k ∂t ∂r 2 (8.42) Equation(8.42)isthediffusivityequationforcompressiblefluids,andithasaverysimilarform toEq.(8.38),whichisthediffusivityequationforslightlycompressiblefluids.TheonlydifferenceintheappearanceofthetwoequationsisthatEq.(8.42)hastherealgaspseudopressure, m(p),substitutedforp.Thereisanothersignificantdifferencethatisnotapparentfromlookingat thetwoequations.Thisdifferenceisintheassumptionconcerningthemagnitudeofthe(∂p/∂r)2 terminEq.(8.41).TolinearizeEq.(8.41),itisnecessarytolimitthetermtoasmallvaluesothat itresultsinanegligiblequantity,whichisnormallythecaseforliquidflowapplications.This limitationisnotnecessaryforthegasequation.Sincepressuregradientsaroundthegaswells canbeverylarge,thetransformationofvariableshasledtoamuchmorepracticalanduseful equationforgases. Equation(8.42)isstillanonlineardifferentialequationbecauseofthedependenceofμ and ctonpressureortherealgaspseudopressure.Thus,thereisnoanalyticalsolutionforEq.(8.42). Al-HussainyandRamey,however,usedfinitedifferencetechniquestoobtainanapproximatesolutiontoEq.(8.42).11Theresultoftheirstudiesforpressuresatthewellbore(i.e.,wherethelogarithmapproximationtotheEifunctioncanbemade)isthefollowingequation: m( pwf ) = m( pi ) − 1637(10 )3 qT kh kt − 3.23 log 2 φμi cti rw (8.43) wherepwfistheflowingpressureatthewellbore;piistheinitialreservoirpressure;qistheflow rateinSCF/dayatstandardconditionsof60°Fand14.7psia;Tisthereservoirtemperaturein°R; kisinmd;hisinft;tisinhr;μiisincpandisevaluatedattheinitialpressure,pi, cti is in psi–1 and isalsoevaluatedatpi;andrwisthewellboreradiusinfeet.Equation(8.43)canbeusedtocalculate theflowingpressureatthesandfaceofagaswell. 8.7 Pseudosteady-State Flow Forthetransientflowcasesthatwereconsideredintheprevioussection,thewellwasassumed tobelocatedinaverylargereservoir.Thisassumptionwasmadesothattheflowfromortothe wellwouldnotbeaffectedbyboundariesthatwouldinhibittheflow.Obviously,thetimethatthis assumptioncanbemadeisafiniteamountandoftenisveryshortinlength.Assoonastheflowbeginstofeeltheeffectofaboundary,itisnolongerinthetransientregime.Atthispoint,itbecomes necessarytomakeanewassumptionthatwillleadtoadifferentsolutiontotheradialdiffusivity equation.Thefollowingsectionsdiscusssolutionstotheradialdiffusivityequationthatallowcalculationsduringthepseudosteady-stateflowregime. Chapter 8 262 • Single-Phase Fluid Flow in Reservoirs 8.7.1 Radial Flow of Slightly Compressible Fluids, Pseudosteady-State Flow Oncethepressuredisturbancehasbeenfeltthroughoutthereservoirincludingattheboundary, the reservoir can no longer be considered as being infinite in size and the flow is not in the transient regime. This situation necessitates another solution to Eq. (8.38), using a different boundary condition at the outer boundary. The initial condition remains the same as before (i.e.,thereservoirpressureispithroughoutthereservoirattimet=0).Theflowrateisagain treatedasconstantatthewellbore.Thenewboundaryconditionusedtofindasolutiontothe radialdiffusivityequationisthattheouterboundaryofthereservoirisano-flowboundary.In mathematicalterms, ∂p = 0at r = re ∂r ApplyingtheseconditionstoEq.(8.38),thesolutionforthepressureatthewellborebecomes pwf = pi − 0.2339 qBt 162.6 qμ B 4A − log 2 kh Ahφ ct 1.781C A rw (8.44) whereAisthedrainageareaofthewellinsquarefeetandCAisareservoirshapefactor.Values oftheshapefactoraregiveninTable8.2forseveralreservoirtypes.Equation(8.44)isvalidonly forsufficientlylongenoughtimesfortheflowtohavereachedthepseudosteady-statetimeperiod. Table 8.2 Shape Factors for Various Single-Well Drainage Areas (after Earlougher3) 1 2 In bounded reservoirs 60º Exact for tDA > Less than 1% error for tDA > Use infinite system solution with less than 1 % error for tDA < ln 2.2458 C A CA ln CA 31.62 3.4538 –1.3224 0.1 0.06 0.10 31.6 3.4532 –1.3220 0.1 0.06 0.10 27.6 3.3178 –1.2544 0.2 0.07 0.09 27.1 3.2995 –1.2452 0.2 0.07 0.09 8.7 Pseudosteady-State Flow 263 1 2 In bounded reservoirs ¹⁄3 Exact for tDA > Less than 1% error for tDA > Use infinite system solution with less than 1 % error for tDA < ln 2.2458 C A CA ln CA 21.9 3.0865 –1.1387 0.4 0.12 0.08 0.098 –2.3227 1.5659 0.9 0.60 0.015 30.8828 3.4302 –1.3106 0.1 0.05 0.09 12.9851 2.5638 –0.8774 0.7 0.25 0.03 4.5132 1.5070 –0.3490 0.6 0.30 0.025 3.3351 1.2045 –0.1977 0.7 0.25 0.01 1 21.8369 3.0836 –1.1373 0.3 0.15 0.025 1 10.8374 2.3830 –0.7870 0.4 0.15 0.025 1 4.5141 1.5072 –0.3491 1.5 0.50 0.06 1 2.0769 0.7309 0.0391 1.7 0.50 0.02 1 3.1573 1.1497 –0.1703 0.4 0.15 0.005 { 1 4 3 2 2 2 2 2 Chapter 8 264 • Single-Phase Fluid Flow in Reservoirs Afterreachingpseudosteady-stateflow,thepressureateverypointinthereservoirischangingatthesamerate,whichsuggeststhattheaveragereservoirpressureisalsochangingatthesame rate.Thevolumetricaveragereservoirpressure,whichisusuallydesignatedas p andisthepressureusedtocalculatefluidpropertiesinmaterialbalanceequations,isdefinedas n p= ∑ p jV j j =1 n (8.45) ∑ Vj j =1 wherepjistheaveragepressureinthejthdrainagevolumeandVjisthevolumeofthejthdrainage volume.ItisusefultorewriteEq.(8.44)intermsoftheaveragereservoirpressure, p : pwf = p − 162.6 qμ B 4A log 2 kh 1.781C A rw (8.46) Forawellinthecenterofacircularreservoirwithadistancetotheouterboundaryofre,Eq.(8.46) reducesto pwf = p − 70.6 qμ B re2 ln 2 − 1.5 kh rw Ifthisequationisrearrangedandsolvedforq, q= 8.7.2 p − pwf 0.00708 kh μB 1n(re / rw ) − 0.75 (8.47) Radial Flow of Compressible Fluids, Pseudosteady-State Flow Thedifferentialequationfortheflowofcompressiblefluidsintermsoftherealgaspseudopressure wasderivedinEq.(8.42).WhentheappropriateboundaryconditionsareappliedtoEq.(8.42),the pseudosteady-statesolutionrearrangedandsolvedforqyieldsEq.(8.48): q= 8.8 19.88(10 )−6 khTsc Tpsc m ( p ) − m( pwf ) ln(re / rw ) − 0.75 (8.48) Productivity Index (PI) Theratiooftherateofproduction,expressedinSTB/dayforliquidflow,tothepressuredrawdown atthemidpointoftheproducinginterval,iscalledtheproductivity index,symbolJ. 8.8 Productivity Index (PI) 265 J= q p − pwf (8.49) Theproductivityindex(PI)isameasureofthewellpotential,ortheabilityofthewelltoproduce, andisacommonlymeasuredwellproperty.TocalculateJfromaproductiontest,itisnecessary toflowthewellasufficientlylongtimetoreachpseudosteady-stateflow.Onlyduringthisflowregimewillthedifferencebetween p and pwfbeconstant.Itwaspointedoutinsection8.3thatonce thepseudosteady-stateperiodhadbeenreached,thepressurechangesateverypointinthereservoir atthesamerate.Thisisnottruefortheotherperiods,andacalculationofproductivityindexduring otherperiodswouldnotbeaccurate. Insomewells,thePIremainsconstantoverawidevariationinflowratesuchthattheflowrate isdirectlyproportionaltothebottom-holepressuredrawdown.Inotherwells,athigherflowratesthe linearityfails,andthePIindexdeclines,asshowninFig.8.15.Thecauseofthisdeclinemaybe(1) turbulenceatincreasedratesofflow,(2)decreaseinthepermeabilitytooilduetopresenceoffreegas causedbythedropinpressureatthewellbore,(3)increaseinoilviscositywithpressuredropbelow bubblepoint,and/or(4)reductioninpermeabilityduetoformationcompressibility. Indepletionreservoirs,theproductivityindicesofthewellsdeclineasdepletionproceeds, owingtotheincreaseinoilviscosityasgasisreleasedfromsolutionandtothedecreaseinthe permeability of the rock to oil as the oil saturation decreases. Since each of these factors may changefromafewtoseveralfoldduringdepletion,thePImaydeclinetoasmallfractionofthe initialvalue.Also,asthepermeabilitytooildecreases,thereisacorrespondingincreaseinthe permeabilitytogas,whichresultsinrisinggas-oilratios.Themaximumrateatwhichawellcan 1.2 600 PI 1.0 0.8 400 te 300 ow 0.6 ra Fl 200 0.4 100 0.2 0 0 0 200 400 Pressure drawdown, psi Figure 8.15 Decline in productivity index at higher flow rates. 600 Productivity index, BPD/psi Flow rate, STB/day 500 Chapter 8 266 • Single-Phase Fluid Flow in Reservoirs producedependsontheproductivityindexatprevailingreservoirconditionsandontheavailable pressuredrawdown.Iftheproducingbottom-holepressureismaintainednearzerobykeepingthe well“pumpedoff,”thentheavailabledrawdownistheprevailingreservoirpressureandthemaximumrateis p × J . Inwellsproducingwater,thePI,whichisbasedondryoilproduction,declinesasthewatercutincreasesbecauseofthedecreaseinoilpermeability,eventhoughthereisnosubstantialdrop inreservoirpressure.Inthestudyofthese“waterwells,”itissometimesusefultoplacethePIon thebasisoftotalflow,includingbothoilandwater,whereinsomecasesthewatercutmayriseto 99%ormore. Theinjectivity indexisusedwithsaltwaterdisposalwellsandwithinjection wellsforsecondaryrecoveryorpressuremaintenance.ItistheratiooftheinjectionrateinSTBperdaytothe excesspressureabovereservoirpressurethatcausesthatinjectionrate,or Injectivityindex= I = q STB/day/psi pwf − p (8.50) Withbothproductivityindexandinjectivityindex,thepressuresreferredtoaresandfacepressures, sothatfrictionalpressuredropsinthetubingorcasingarenotincluded.Inthecaseofinjectingor producingathighrates,thesepressurelossesmaybeappreciable. Incomparingonewellwithanotherinagivenfield,particularlywhenthereisavariationin netproductivethicknessbutwhentheotherfactorsaffectingtheproductivityindexareessentially thesame,thespecificproductivityindexJsissometimesused,whichistheproductivityindexdividedbythenetfeetofpay,or 8.8.1 Specificproductivityindex = J s = J q STB/day/psi/ft = h h( p − pwf ) (8.51) Productivity Ratio (PR) Inevaluatingwellperformance,thestandardusuallyreferredtoistheproductivityindexofanopen holethatcompletelypenetratesacircularformationnormaltothestrataandinwhichnoalterationin permeabilityhasoccurredinthevicinityofthewellbore.SubstitutingEq.(8.47)intoEq.(8.49),weget J = 0.00708 kh μ B(1n(re / rw ) − 0.75 ) (8.52) Theproductivityratio(PR)thenistheratioofthePIofawellinanyconditiontothePIofthis standardwell: PR = J J sw (8.53) 8.9 Superposition 267 Thus,theproductivityratiomaybelessthanone,greaterthanone,orequaltoone.Althoughthe productivityindexofthestandardwellisgenerallyunknown,therelativeeffectofcertainchanges inthewellsystemmaybeevaluatedfromtheoreticalconsiderations,laboratorymodels,orwell tests.Forexample,thetheoreticalproductivityratioofawellreamedfroman8-in.boreholediameterto16in.isderivedbyEq.(8.52): PR = J16 ln (re / 0.333) − 0.75 = J 8 ln (re / 0.667 ) − 0.75 Assumingre=660ft, PR = ln (660 / 0.333) − 0.75 = 1.11 ln (660 / 0.667 ) − 0.75 Thus,doublingtheboreholediametershouldincreasethePIapproximately11%.Aninspectionof Eq.(8.50)indicatesthatthePIcanbeimprovedbyincreasingtheaveragepermeabilityk,decreasingtheviscosityμ,orincreasingthewellboreradiusrw.Anothernamefortheproductivityratiois theflow efficiency (FE). 8.9 Superposition Earlougherandothershavediscussedtheapplicationoftheprincipleofsuperpositiontofluid flowinreservoirs.3,12,13,14Thisprincipleallowstheuseoftheconstantrate,single-wellequations thathavebeendevelopedearlierinthischapterandappliesthemtoavarietyofothercases.To illustratetheapplication,thesolutiontoEq.(8.38),whichisalinear,second-orderdifferential equation,isexamined.Theprincipleofsuperpositioncanbestatedasfollows:Theadditionof solutions to a linear differential equation results in a new solution to the original differential equation.Forexample,considerthereservoirsystemdepictedinFig.8.16.Intheexampleshown inFig.8.16,wells1and2areopeneduptotheirrespectiveflowrates,q1 and q2,andthepressure dropthatoccursintheobservationwellismonitored.Theprincipleofsuperpositionstatesthat thetotalpressuredropwillbethesumofthepressuredropcausedbytheflowfromwell1and thepressuredropcausedbytheflowfromwell2: Δpt = Δp1 + Δp2 EachoftheindividualΔptermsisgivenbyEq.(8.39),or Δp = pi – p(r, t)= 70.6 qμ B φμ ct r 2 − Ei − kh 0.00105 kt Chapter 8 268 • Single-Phase Fluid Flow in Reservoirs Observation well r1 r2 Well 1 Well 2 Figure 8.16 Two flowing-well reservoir system to illustrate the principle of superposition. Toapplythemethodofsuperposition,pressuredropsorchangesareadded.Itisnotcorrectsimply toaddorsubtractindividualpressureterms.Itisobviousthatiftherearemorethantwoflowing wellsinthereservoirsystem,theprocedureisthesame,andthetotalpressuredropisgivenbythe following: N Δp j = ∑ Δp j (8.54) j =1 whereNequalsthenumberofflowingwellsinthesystem.Example8.2illustratesthecalculations involvedwhenmorethanonewellaffectsthepressureofapointinareservoir. Example 8.2 Calculating Total Pressure Drop ForthewelllayoutshowninFig.8.17,calculatethetotalpressuredropasmeasuredintheobservationwell(well3)causedbythefourflowingwells(wells1,2,4,and5)after10days.The wellswereshutinforalongtimebeforeopeningthemtoflow. Given Thefollowingdataapplytothereservoirsystem: µ=0.40cp Bo=1.50bbl/STB k =47md h=50ft 8.9 Superposition 269 5 1 17 90 ' 00 16 ' 3 18 ' 20 70 19 ' Flowing well 4 2 Observation well Figure 8.17 Well layout for Problem 8.2. φ=11.2% ct=15×10–6 psi–1 Well Flow rate (STB/day) Distance to observation well (feet) 1 265 1700 2 270 1920 4 287 1870 5 260 1690 Solution TheindividualpressuredropscanbecalculatedwithEq.(8.39),andthetotalpressuredropisgiven byEq.(8.54).Forwell1, p(r, t ) = pi − Δp1 = 70.6 qμ B φμ ct r 2 − Ei − kh 0.00105 kt (.112 )(0.40 )(15 × 10 −6 )(1700 )2 70.6(265 )(0.40 )(1.5 ) − Ei − 0.00105( 47 )(240 ) ( 47 )(50 ) Δp1=4.78[–Ei(–0.164)] FromFig.8.12, – Ei(–0.164)=1.39 (8.36) Chapter 8 270 • Single-Phase Fluid Flow in Reservoirs Therefore, Δp1=4.78(1.39)=6.6psi Similarly,forwells2,4,and5, Δp2=4.87[–Ei(–0.209)]=5.7psi Δp4=5.14[–Ei(–0.198)]=6.4psi Δp5=4.69[–Ei(–0.162)]=6.6psi UsingEq.(8.54)tofindthetotalpressuredropattheobservationwell(well3),theindividual pressuredropsareaddedtogethertogivethetotal: Δpt = Δp1 + Δp2 + Δp4 + Δp5 or Δpt=6.6+5.7+6.4+6.6=25.3psi Thesuperpositionprinciplecanalsobeappliedinthetimedimension,asisillustratedin Fig.8.18.Inthiscase,onewell(whichmeansthepositionwherethepressuredisturbancesoccur remainsconstant)hasbeenproducedattwoflowrates.Thechangeintheflowratefromq1toq2occurredattimet1.Figure8.18showsthatthetotalpressuredropisgivenbythesumofthepressure dropcausedbytheflowrate,q1,andthepressuredropcausedbythechangeinflowrate,q2 – q1. Thisnewflowrate,q2 – q1,hasflowedfortimet – t1. Thepressuredropforthisflowrate,q2 – q1,isgivenby Δp = pi – p (r, t)= 70.6(q2 − q1 )μ B φμ ct r 2 − Ei kh 0.00105 k (t − t1 ) Asinthecaseofthemultiwellsystemjustdescribed,superpositioncanalsobeappliedtomultirate systemsaswellasthetworateexamplesdepictedinFig.8.18. 8.9.1 Superposition in Bounded or Partially Bounded Reservoirs AlthoughEq.(8.39)appliestoinfinitereservoirs,itmaybeusedinconjunctionwiththesuperpositionprincipletosimulateboundariesofclosedorpartiallyclosedreservoirs.Theeffect ofboundariesisalwaystocausegreaterpressuredropsthanthosecalculatedfortheinfinite Superposition 271 q2 Production rate, q 8.9 q2 – q1 q1 t1 Flowing well pressure, Pwl Time Pi Pressure drop due to well flowing at rate q1 Additional pressure drop due to well flowing at rate q2 – q1 t1 Time Figure 8.18 Production rate and pressure history for a well with two flow rates. reservoirs.Themethodofimagesisusefulinhandlingtheeffectofboundaries.Forexample, thepressuredropatpointx(Fig.8.19),owingtoproductioninawelllocatedadistancedfrom asealingfault,willbethesumoftheeffectsoftheproducingwellandanimagewellthatis superimposedatadistancedbehindthefault.Inthiscase,thetotalpressuredropisgivenby Eq.(8.54),wheretheindividualpressuredropsareagaingivenbyEq.(8.39),orforthecase showninFig.8.19, Δp = Δp1 + Δpimage Δp1 = φμ ct r12 70.6 qμ B − Ei kh −0.00105 kt Δpimage = φμ ct r22 70.6 qμ B − Ei kh −0.00105 kt Chapter 8 272 • d Well Single-Phase Fluid Flow in Reservoirs d Image well r1 x Fault r2 Figure 8.19 Method of images used in the solution of boundary problems. 8.10 Introduction to Pressure Transient Testing Pressuretransienttestingisanimportantdiagnostictoolthatcanprovidevaluableinformationfor thereservoirengineer.Atransienttestisinitiatedbycreatingadisturbanceatawellbore(i.e.,a changeintheflowrate)andthenmonitoringthepressureasafunctionoftime.Anefficientlyconductedtestthatyieldsgooddatacanprovideinformationsuchasaveragepermeability,drainage volume,wellboredamageorstimulation,andreservoirpressure. Apressuretransienttestdoesnotalwaysyieldauniquesolution.Thereareoftenanomalies associatedwiththereservoirsystemthatyieldpressuredatathatcouldleadtomultipleconclusions.Inthesecases,thestrengthoftransienttestingisrealizedonlywhentheprocedureisusedin conjunctionwithotherdiagnostictoolsorotherinformation. Inthenexttwosubsections,thetwomostpopulartests(i.e.,thedrawdownandbuildup tests)areintroduced.However,noticethatthematerialisintendedtobeonlyanintroduction. Thereadermustbeawareofmanyotherconsiderationsinordertoconductapropertransient test.ThereaderisreferredtosomeexcellentbooksinthisareabyEarlougher,Matthewsand Russell,andLee.3,10,15 8.10.1 Introduction to Drawdown Testing Thedrawdowntestconsistsofflowingawellataconstantratefollowingashut-inperiod.The shut-inperiodshouldbesufficientlylongforthereservoirpressuretohavestabilized.Thebasisfor thedrawdowntestisfoundinEq.(8.40), 8.10 Introduction to Pressure Transient Testing p(r, t ) = pi − 162.6 qμ B kt − 3.23 log 2 kh ϕμ ct r 273 (8.40) whichpredictsthepressureatanyradius,r,asafunctionoftimeforagivenreservoirflowsystem duringthetransientperiod.Ifr = rw,thenp(r, t)willbethepressureatthewellbore.Foragiven reservoirsystem,pi, q, μ, B, k, h, φ, ct, and rwareconstant,andEq.(8.40)canbewrittenas pwf = b + mlog(t) (8.55) where pwf=flowingwellpressureinpsia b=constant t=timeinhrs 162.6 qμ B m=constant= − kh (8.56) Equation(8.55)suggeststhataplotofpwfversustonsemiloggraphpaperwouldyieldastraightline withslopemthroughtheearlytimedatathatcorrespondwiththetransienttimeperiod.Thisisproviding thattheassumptionsinherentinthederivationofEq.(8.40)aremet.Theseassumptionsareasfollows: 1. Laminar,horizontalflowinahomogeneousreservoir 2. Reservoirandfluidproperties,k, φ, h, ct, μ, and B,independentofpressure 3. Single-phaseliquidflowinthetransienttimeregion 4. Negligiblepressuregradients Theexpressionfortheslope,Eq.(8.56),canberearrangedtosolveforthecapacity, kh,ofthe drainageareaoftheflowingwell.Ifthethicknessisknown,thentheaveragepermeabilitycanbe obtainedbyEq.(8.57): k=− 162.6 qμ B mh (8.57) Ifthedrawdowntestisconductedlongenoughforthepressuretransientstoreachthepseudosteady-stateperiod,thenEq.(8.55)nolongerapplies. 8.10.2 Drawdown Testing in Pseudosteady-State Regime Inthepseudosteady-stateregime,Eq.(8.44)isusedtodescribethepressurebehavior: pwf = pi − 0.2339 qBt 162.6 qμ B 4A − log 2 kh Ahφ ct 1.781C A rw (8.44) Chapter 8 274 • Single-Phase Fluid Flow in Reservoirs Again,groupingtogetherthetermsthatareconstantforagivenreservoirsystem,Eq.(8.44)becomes pwf = b′ + m′t (8.58) where b′=constant 0.2339 qB m′=constant = − Ahφ ct (8.59) NowaplotofpressureversustimeonregularCartesiangraphpaperyieldsastraightlinewithslope equaltom′throughthelatetimedatathatcorrespondtothepseudosteady-stateperiod.IfEq.(8.59) isrearranged,anexpressionforthedrainagevolumeofthetestwellcanbeobtained: Ahφ = − 8.10.3 0.2339 qB m ' ct (8.60) Skin Factor Thedrawdowntestcanalsoyieldinformationaboutdamagethatmayhaveoccurredaroundthewellboreduringtheinitialdrillingorduringsubsequentproduction.Anequationwillnowbedeveloped thatallowsthecalculationofadamagefactor,usinginformationfromthetransientflowregion. Adamagezoneyieldsanadditionalpressuredropbecauseofthereducedpermeabilityin thatzone.VanEverdingenandHurstdevelopedanexpressionforthispressuredropanddefineda dimensionlessdamagefactor,S,calledtheskinfactor:16,17 Δpskin = 141.2 qμ B S kh (8.61) or Δpskin=–0.87mS (8.62) FromEq.(8.62),apositivevalueofScausesapositivepressuredropandthereforerepresentsa damagesituation.AnegativevalueofScausesanegativepressuredropthatrepresentsastimulated conditionlikeafracture.Noticethatthesepressuredropscausedbytheskinfactorarecompared to the pressure drop that would normally occur through this affected zone as predicted by Eq. (8.40).CombiningEqs.(8.40)and(8.62),thefollowingexpressionisobtainedforthepressureat thewellbore: pwf = pi − 162.6 qμ B kt − 3.23 + 0.87 S log 2 kh φμ ct rw (8.63) 8.10 Introduction to Pressure Transient Testing 275 Thisequationcanberearrangedandsolvedfortheskinfactor,S: pi − pwf 162.6 qμ B kt S = 1.151 − log + . 3 23 kh φμ ct rw2 The value of pwf must be obtained from the straight line in the transient flow region. Usually a timecorrespondingto1hrisused,andthecorrespondingpressureisgivenbythedesignationp1hr. Substitutingmintothisequationandrecognizingthatthedenominatorofthefirsttermwithinthe bracketsisactually–m, p − pi k S = 1.151 1hr − log + 3.23 2 φμ ct rw m (8.64) Equation(8.64)canbeusedtocalculateavalueforSfromtheslopeofthetransientflowregion andthevalueofp1hralsotakenfromthestraightlineinthetransientperiod. A drawdown test is often conducted during the initial production from a well, since the reservoirhasobviouslybeenstabilizedattheinitialpressure,pi.Thedifficultaspectofthetestis maintainingaconstantflowrate,q.Iftheflowrateisnotkeptconstantduringthelengthofthetest, thenthepressurebehaviorwillreflectthisvaryingflowrateandthecorrectstraightlineregions onthesemilogandregularCartesianplotsmaynotbeidentified.Otherfactorssuchaswellbore storage(shut-inwell)orunloading(flowingwell)caninterferewiththeanalysis.Wellborestorage andunloadingarephenomenathatoccurineverywelltoacertaindegreeandcauseanomaliesin thepressurebehavior.Wellborestorageiscausedbyfluidflowingintothewellboreafterawell hasbeenshutinonthesurfaceandbythepressureinthewellborechangingastheheightofthe fluidinthewellborechanges.Wellboreunloadinginaflowingwellwillleadtomoreproduction atthesurfacethanwhatactuallyoccursdownhole.Theeffectsofwellborestorageandunloading canbesodominatingthattheycompletelymaskthetransienttimedata.Ifthishappensandifthe engineerdoesnotknowhowtoanalyzefortheseeffects,thepressuredatamaybemisinterpreted anderrorsincalculatedvaluesofpermeability,skin,andthelikemayoccur.Wellborestorageand unloadingeffectsarediscussedindetailbyEarlougher.3Theseeffectsshouldalwaysbetakeninto considerationwhenevaluatingpressuretransientdata. Thefollowingexampleproblemillustratestheanalysisofdrawdowntestdata. Example 8.3 Calculating Average Permeability, Skin Factor, and Drainage Area Adrawdowntestwasconductedonanewoilwellinalargereservoir.Atthetimeofthetest,the wellwastheonlywellthathadbeendevelopedinthereservoir.Analysisofthedataindicatesthat wellborestoragedoesnotaffectthepressuremeasurements.Usethedatatocalculatetheaverage permeabilityoftheareaaroundthewell,theskinfactor,andthedrainageareaofthewell. Chapter 8 276 • Single-Phase Fluid Flow in Reservoirs Given pi=4000psia h=20ft q=500STB/day ct=30×10–6 psia–1 μo=1.5cp φ=25% Bo=1.2bbl/STB rw=0.333ft Flowing pressure, pwf (psia) Time, t (hrs) 3503 2 3469 5 3443 10 3417 20 3383 50 3368 75 3350 100 3317 150 3284 200 3220 300 Solution Figure8.20containsasemilogplotofthepressuredata.Theslopeoftheearlytimedata,whichare inthetransienttimeregion,is–86psi/cycle,andthevalueofP1hrisreadfromthepressurevalueon thelineat1hras3526psia.Equation(8.57)cannowbeusedtocalculatethepermeability: k=− k=− 162.6 qμ B mh (8.57) 162.6(500 )(1.5 )(1.2 ) = 85.1 md −86(20 ) TheskinfactorisfoundfromEq.(8.64): p − pi k S = 1.151 1hr − log + 3.23 2 m φμ c r t w (8.64) 8.10 Introduction to Pressure Transient Testing 277 3550 P1hr = 3526 psia 3500 Pressure 3450 Slope = –86 psi/cycle 3400 3350 3300 3250 3200 0 0.5 1.0 1.5 Log t 2.0 2.5 3.0 Figure 8.20 Plot of pressure versus log time for the data of Example 8.3. 3526 − 4000 85.1 + 3.23 S = 1.151 − log 2 −6 − 86 ( . )( . )( )( 0 25 1 5 30 10 ( 0 . 333 ) × S=1.04 Thispositivevaluefortheskinfactorsuggeststhewellisslightlydamaged. FromtheslopeofaplotofPversustimeonregularCartesiangraphpaper,showninFig.8.21, andusingEq.(8.60),anestimateforthedrainageareaofthewellcanbeobtained.Fromthesemilogplotofpressureversustime,thefirstsixdatapointsfellonthestraightlineregionindicating theywereinthetransienttimeperiod.Therefore,thelasttwotothreepointsofthedataareinthe pseudosteady-stateperiodandcanbeusedtocalculatethedrainagearea.Theslopeofalinedrawn throughthelastthreepointsis–0.650.Therefore, Ahφ = − A=− 8.10.4 0.2339 qB m ' ct (8.60) 0.2339(500 )(1.2 ) = 1, 439, 000 ft 2 = 33.0 ac ( −.650 )( 30 × 10 )−6 (20 )(0.25 ) Introduction to Buildup Testing Thebuilduptestisthemostpopulartransienttestusedintheindustry.Itisconductedbyshutting inaproducingwellthathasobtainedastabilizedpressureinthepseudosteady-statetimeregion Chapter 8 278 • Single-Phase Fluid Flow in Reservoirs 3550 3500 Pressure 3450 3400 3350 3300 m' = 0.650 3250 3200 0 50 100 150 200 250 300 350 Time Figure 8.21 Plot of pressure versus time for the data of Example 8.3. byflowingthewellataconstantrateforasufficientlylongperiod.Thepressureisthenmonitored duringthelengthoftheshut-inperiod.Theprimaryreasonforthepopularityofthebuilduptestis thefactthatitiseasytomaintaintheflowrateconstantatzeroduringthelengthofthetest.The maindisadvantageofthebuilduptestoverthatofthedrawdowntestisthatthereisnoproduction duringthetestandthereforenosubsequentincome. Apressurebuilduptestissimulatedmathematicallybyusingtheprincipleofsuperposition. Beforetheshut-inperiod,awellisflowedataconstantflowrate,q.Atthetimecorrespondingto thepointofshut-in,tp,asecondwell,superimposedoverthelocationofthefirstwell,isopened toflowatarateequalto–q,whilethefirstwellisallowedtocontinuetoflowatrateq.Thetime thatthesecondwellisflowedisgiventhesymbolofΔt.Whentheeffectsofthetwowellsare added,theresultisthatawellhasbeenallowedtoflowatrateqfortimetpandthenshutinfor timeΔt.Thissimulatestheactualtestprocedure,whichisshownschematicallyinFig.8.22.The timecorrespondingtothepointofshut-in,tp,canbeestimatedfromthefollowingequation: tp = Np q (8.65) whereNp=cumulativeproductionthathasoccurredduringthetimebeforeshut-inthatthewell wasflowedattheconstantflowrateq. Equations(8.40)and(8.54)canbeusedtodescribethepressurebehavioroftheshut-inwell: pws = pi − k (t p + Δt ) 1662.6( − q )μ B 162.qμ B k Δt − 3.23 − − 3.23 log log 2 2 kh kh φμ ct rw φμ ct rw 8.10 Introduction to Pressure Transient Testing 279 Flow rate q 0 –q Time Time Flow rate q 0 Time Figure 8.22 Graphical simulation of pressure buildup test using superposition. Expandingthisequationandcancelingterms, pws = pi − (t p + Δt ) 162.qμ B log Δt kh (8.66) where pws = bottom-hole shut-in pressure Equation(8.66)isusedtocalculatetheshut-inpressureasafunctionoftheshut-intimeandsuggests thataplotofthispressureversustheratioof(tp + Δt)/Δtonsemiloggraphpaperwillyieldastraight line.ThisplotisreferredtoasaHorner plot,afterthemanwhointroduceditintothepetroleumliterature.18Figure8.23isanexampleofaHornerPlot.Thepointsontheleftoftheplotconstitutethe linearportion,whilethetwopointstotheright,representingtheearlytimedata,areseverelyaffected bywellborestorageeffectsandshouldbedisregarded.TheslopeoftheHornerplotisequaltom, or m=− 162.6 qμ B kh Thisequationcanberearrangedtosolveforthepermeability: k=− 162.6 qμ B mh (8.67) Chapter 8 280 • Single-Phase Fluid Flow in Reservoirs 2800 2700 Pressure 2600 2500 y = –94.236x + 2746.4 2400 2300 2200 0 0.5 1.0 1.5 log ((tp + ∆t)/∆t) 2.0 2.5 Figure 8.23 Plot of pressure versus time ratio for Example 8.4. TheskinfactorequationforbuildupisfoundbycombiningEq.(8.64),writtenfort = tp(Δt=0), andEq.(8.66): pwf ( Δt = 0 ) − pws kt p Δt S = 1.151 − log + 3.23 2 m φμ ct rw (t p + Δt ) Theshut-inpressure,pws,canbetakenatanyΔtonthestraightlineofthetransientflowperiod.For convenience,Δtissetequalto1hr,andpwsistakenfromthestraightlineatthatpoint.Thevaluefor p1hrmustbeonthestraightlineandmightnotbeadatapoint.AtatimeofΔt=1hr,tpismuchlarger thanΔtformosttests,andtp + Δt ≈ tp.Withtheseconsiderations,theskinfactorequationbecomes pwf ( Δt = 0 ) − p1hr k S = 1.151 − log + 3.23 2 m c r φμ t w (8.68) Thissectionisconcludedwithanexampleproblemillustratingtheanalysisofabuilduptest. Notice again that there is much more to this overall area of pressure transient testing. Pressure transienttestingisaveryusefulquantitativetoolforthereservoirengineerifusedcorrectly.The intentofthissectionwassimplytointroducetheseimportantconcepts.Thereadershouldpursue theindicatedreferencesifmorethoroughcoverageofthematerialisneeded. 8.10 Introduction to Pressure Transient Testing Example 8.4 281 Calculating Permeability and Skin from a Pressure Buildup Test Given Flowratebeforeshutinperiod=280STB/day Npduringconstantrateperiodbeforeshutin=2682STB pwfatthetimeofshut-in=1123psia FromtheforegoingdataandEq.(8.65),tpcanbecalculated: tp = 2682 = 24 = 230hrs 280 q Np Othergivendataare Bo=1.31bbl/STB μo=2.0cp h=40ft ct=15×10–6 psi–1 φ=10% rw=0.333ft Time after shut in, Δt (hours) Pressure, pws (psia) t p + Δt Δt 2 2290 116.0 4 2514 58.5 8 2584 29.8 12 2612 20.2 16 2632 15.4 20 2643 12.5 24 2650 10.6 30 2658 8.7 Solution Theslopeofthestraight-lineregion(noticethedifficultyinidentifyingthestraight-lineregion)of theHornerplotinFig.8.23is–94.23psi/cycle.FromEq.(8.67), k=− 162.6 qμ B mh (8.67) Chapter 8 282 k=− • Single-Phase Fluid Flow in Reservoirs 162.6(280 )(2.0 )(1.31) = 31md ( −94.23)( 40 ) AgainfromtheHornerplot,p1hris2523psiaand,fromEq.(8.68), pwf ( Δt = 0 ) − p1hr k S = 1.151 − log + 3.23 2 m φμ ct rw (8.68) 1123 − 2523 31 + 3.23 S = 1.151 − log 2 −6 . − 94 23 0 1 2 0 15 10 ( 0 . 333 ) ( . )( . )( )( × S=11.64 TheextrapolationofthestraightlinetotheHornertimeequalto1providestheextrapolatedpressure,p*.Foranewwell,p*providesanestimatefortheinitialreservoirpressure,pi. Thetimeratio(tp + Δt)/ΔtdecreasesasΔtincreases.Therefore,theearlytimedataare ontherightandthelatetimedataontheleftofFig.8.23.Becausemostofthedatapointsare influencedbywellborestorage,itisdifficulttoidentifythecorrectstraightlineofthetransienttimeregion.Forthisexampleproblem,thelastthreedatapointswereusedtorepresent thetransienttimeregion.Thisdifficultyinidentifyingtheproperstraight-lineregionpoints outtheimportanceofathoroughunderstandingofwellborestorageandotheranomaliesthat couldaffectthepressuretransientdata.Modernpressuretransientinterpretationmethodsin Leeetal.(2004)offermoreeffectivewaystodothisanalysisthatarebeyondthescopeofthis chapter. Problems 8.1 Two wells are located 2500 ft apart.The static well pressure at the top of perforations (9332ftsubsea)inwellAis4365psiaandatthetopofperforations(9672ftsubsea)in wellBis4372psia.Thereservoirfluidgradientis0.25psi/ft,reservoirpermeabilityis 245md,andreservoirfluidviscosityis0.63cp. (a) (b) (c) (d) (e) (f) Correctthetwostaticpressurestoadatumlevelof9100ftsubsea. Inwhatdirectionisthefluidflowingbetweenthewells? Whatistheaverageeffectivepressuregradientbetweenthewells? Whatisthefluidvelocity? Isthisthetotalvelocityoronlythecomponentofthevelocityinthedirectionbetween thetwowells? ShowthatthesamefluidvelocityisobtainedusingEq.(8.1). Problems 283 8.2 Asandbodyis1500ftlong,300ftwide,and12ftthick.Ithasauniformpermeabilityof 345mdtooilat17%connatewatersaturation.Theporosityis32%.Theoilhasareservoir viscosityof3.2cpandBoof1.25bbl/STBatthebubblepoint. (a) Ifflowtakesplaceabovethebubble-pointpressure,whichpressuredropwillcause 100 reservoir bbl/day to flow through the sand body, assuming the fluid behaves essentiallyasanincompressiblefluid?Whichpressuredropwilldosofor200reservoirbbl/day? (b) Whatistheapparentvelocityoftheoilinfeetperdayatthe100-bbl/dayflowrate? (c) Whatistheactualaveragevelocity? (d) Whattimewillberequiredforcompletedisplacementoftheoilfromthesand? (e) Whatpressuregradientexistsinthesand? (f) Whatwillbetheeffectofraisingboththeupstreamanddownstreampressuresby,say, 1000psi? (g) Consideringtheoilasafluidwithaveryhighcompressibilityof65(10)–6 psi–1,how muchgreateristheflowrateatthedownstreamendthantheupstreamendat100bbl/ day? (h) Whatpressuredropwillberequiredtoflow100bbl/day,measuredattheupstream pressure,throughthesandifthecompressibilityoftheoilis65(10)–6 psi–1?Consider theoiltobeaslightlycompressiblefluid (i) Whatwillbethedownstreamflowrate? (j) Whatconclusioncanbedrawnfromthesecalculations,concerningtheuseoftheincompressible flow equation for the flow of slightly compressible liquids, even with highcompressibilities? 8.3 IfthesandbodyofProblem8.2hadbeenagasreservoirwithabottom-holetemperatureof 140°Fbutwiththesameconnatewaterandpermeabilitytogas,thencalculatethefollowing: (a) Withanupstreampressureof2500psia,whatdownstreampressurewillcause5.00MM SCF/daytoflowthroughthesand?Assumeanaveragegasviscosityof0.023cpandan averagegasdeviationfactorof0.88. (b) Whatdownstreampressurewillcause25MMSCF/daytoflowifthegasviscosityand deviationfactorsremainthesame? (c) Explainwhyittakesmorethanfivetimesthepressuredroptocausefivetimesthegasflow. (d) Whatisthepressureatthemidpointofthesandwhen25MMSCF/dayisflowing? (e) Whatisthemeanpressureat25MMSCF/day? (f) Whyisthereagreaterpressuredropinthedownstreamhalfofthesandbodythanin theupstreamhalf? (g) Fromthegaslaw,calculatetherateofflowatthemeanpressurepmandshowthatthe equationintermsofqmisvalidbynumericalsubstitution. Chapter 8 284 • Single-Phase Fluid Flow in Reservoirs 8.4 (a) P lotpressureversusdistancethroughthesandofthepreviousproblematthe25MM SCF/dayflowrate. (b) Plotthepressuregradientversusdistancethroughthesandbody. 8.5 Arectangularsandbodyisflowinggasat10MMSCF/dayunderadownstreampressureof 1000psia.Standardconditionsare14.4psiaand80°F.Theaveragedeviationfactoris0.80. Thesandbodyis1000ftlong,100ftwide,and10ftthick.Porosityis22%andaverage permeabilitytogasat17%connatewateris125md.Bottom-holetemperatureis160°F,and gasviscosityis0.029cp. (a) (b) (c) (d) Whatistheupstreampressure? Whatisthepressuregradientatthemidpointofthesand? Whatistheaveragepressuregradientthroughoutthesand? Wheredoesthemeanpressureoccur? 8.6 Ahorizontalpipe10cmindiameterand3000cmlongisfilledwithasandof20%porosity. Ithasaconnatewatersaturationof30%and,atthatwatersaturation,apermeabilityofoil of200md.Theviscosityoftheoilis0.65cp,andthewaterisimmobile. (a) Whatistheapparentvelocityoftheoilundera100-psipressuredifferential? (b) Whatistheflowrate? (c) Calculatetheoilcontainedinthepipeandthetimeneededtodisplaceitattherateof 0.055cm3/sec. (d) Fromthisactualtimeandthelengthofthepipe,calculatetheactualaveragevelocity. (e) Calculatetheactualaveragevelocityfromtheapparentvelocity,porosity,andconnate water. (f) Whichvelocityisusedtocalculateflowrates,andwhichisusedtocalculatedisplacementtimes? (g) Iftheoilisdisplacedwithwatersothat20%unrecoverable(orresidual)oilsaturation isleftbehindthewaterfloodfront,whataretheapparentandactualaveragevelocities inthewateredzonebehindthefloodfrontiftheoilproductionrateismaintainedat 0.055cm3/sec?Assumepiston-likedisplacementoftheoilbythewater. (h) Whatistherateofadvanceofthefloodfront? (i) Howlongwillittaketoobtainalltherecoverableoil,andhowmuchwillberecovered? (j) Howmuchpressuredropwillberequiredtoproduceoilattherateof0.055cm3/sec whenthewaterfloodfrontisatthemidpointofthepipe? 8.7 (a) T hreebedsofequalcrosssectionhavepermeabilitiesof50md,500md,and200md andlengthsof10ft,40ft,and75ft,respectively.Whatistheaveragepermeabilityof thebedsplacedinseries? (b) Whataretheratiosofthepressuredropsacrosstheindividualbedsforliquidflow? Problems 285 (c) Forgasflow,willtheoverallpressuredropthroughbedsinseriesbethesameforflow ineitherdirection?Willtheindividualpressuredropsbethesame? (d) Thegasflowconstantforagivenlinearsystemis900,sothat p12 – p22 =900L/k.If the upstream pressure is 500 psia, calculate the pressure drops in each of two beds forseriesflowinbothdirections.Theonebedis10ftlongand100md;thesecondis 70ftand900md. (e) Aproducingformationfromtoptobottomconsistsof10ftof350mdsand,4in.of 0.5mdshale,4ftof1230mdsand,2in.of2.4mdshale,and8ftof520mdsand.What istheaverageverticalpermeability? (f) Ifthe8ftof520mdsandisinthelowerpartoftheformationandcarrieswater,what wellcompletiontechniquewillyouusetokeepthewater-oilratiolowforthewell? Discusstheeffectofthemagnitudeofthelateralextentoftheshalebreaksonthewell production. 8.8 (a) T hreebedsthatare40md,100md,and800mdand4,6,and10ftthick,respectively, areconductingfluidinparallelflow.Ifallareofequallengthandwidth,whatisthe averagepermeability? (b) Inwhatratioaretheseparateflowsinthethreebeds? 8.9 As project supervisor for an in situ uranium leaching project, you have observed that to maintainaconstantinjectionrateinwellA,thepumppressurehadtobeincreasedsothat pe – pwwasincreasedbyafactorof20fromthevalueatstartup.Anaveragepermeabilityof 100mdwasmeasuredfromplugscoredbeforetheinjectionofleachant.Yoususpectbuildupofacalciumcarbonateprecipitatehasdamagedtheformationneartheinjectionwell.If thepermeabilityofthedamagedsectioncanbeassumedtobe1md,findtheextentofthe damage.Thewellboreradiusis0.5ft,andthedistancetotheouterboundaryoftheuranium depositisestimatedtobe1000ft. 8.10 Awellwasgivenalargefracturetreatment,creatingafracturethatextendstoaradiusofabout 150ft.Theeffectivepermeabilityofthefractureareawasestimatedtobe200md.Thepermeabilityoftheareabeyondthefractureis15md.Assumethattheflowissteadystate,singlephase, andincompressible.Theouterboundaryatr = re=1500fthasapressureof2200psia,andthe wellborepressureis100psia(rw=0.5ft).Thereservoirthicknessis20ftandtheporosityis 18%.Theflowingfluidhasaformationvolumefactorof1.12bbl/STBandaviscosityof1.5cp. (a) CalculatetheflowrateinSTB/day. (b) Calculatethepressureinthereservoiratadistanceof300ftfromthecenterofthe wellbore. 8.11 (a) A limestone formation has a matrix (primary or intergranular) permeability of less than1md.However,itcontains10solutionchannelspersquarefoot,each0.02in.in 286 Chapter 8 • Single-Phase Fluid Flow in Reservoirs diameter.Ifthechannelslieinthedirectionoffluidflow,whatisthepermeabilityof therock? (b) Iftheporosityofthematrixrockis10%,whatpercentageofthefluidisstoredintheprimaryporesandwhatpercentageisstoredinthesecondarypores(vugs,fractures,etc.)? (c) Ifthesecondaryporesystemiswellconnectedthroughoutareservoir,whatconclusionsmustbedrawnconcerningtheprobableresultofgasorwaterdriveontherecoveryofeitheroil,gas,orgascondensate?What,then,arethemeansofrecoveringthe hydrocarbonsfromtheprimarypores? 8.12 Duringagravelrockoperation,the6-in.(indiameter)linerbecamefilledwithgravel,and alayerofmillscaleanddirtaccumulatedtoathicknessof1in.ontopofthegravelwithin thepipe.Ifthepermeabilityoftheaccumulationis1000md,whatadditionalpressuredrop isplacedonthesystemwhenpumpinga1-cpfluidattherateof100bbl/hr? 8.13 One hundred capillary tubes of 0.02 in. in diameter and 50 capillary tubes of 0.04 in. (indiameter),allofequallength,areplacedinsideapipeof2in.indiameter.Thespace betweenthetubesisfilledwithwaxsothatflowisonlythroughthecapillarytubes.Whatis thepermeabilityofthis“rock”? 8.14 Suppose,aftercementing,anopening0.01in.wideisleftbetweenthecementandan8-in. diameterhole.Ifthiscircularfractureextendsfromtheproducingformationthroughan impermeableshale20ftthicktoanunderlyingwatersand,atwhatratewillwaterenter theproducingformation(well)undera100-psipressuredrawdown?Thewatercontains 60,000ppmsaltandthebottom-holetemperatureis150°F. 8.15 Ahighwater-oilratioisbeingproducedfromawell.Itisthoughtthatthewateriscoming fromanunderlyingaquifer20ftfromtheoil-producingzone.Inbetweentheaquiferandthe producingzoneisanimpermeableshalezone.Assumethatthewateriscomingupthrough anincompletecementingjobthatleftanopening0.01in.widebetweenthecementandthe 8in.hole.Thewaterhasaviscosityof0.5cp.Determinetherateatwhichwaterisentering thewellattheproducingformationlevelifthepressureintheaquiferis150psigreaterthan thepressureinthewellattheproducingformationlevel. 8.16 Derivetheequationforthesteady-state,semisphericalflowofanincompressiblefluid. 8.17 Awellhasashut-inbottom-holepressureof2300psiaandflows215bbl/dayofoilundera drawdownof500psi.Thewellproducesfromaformationof36ftnetproductivethickness. Use rw = 6 in., re=660ft,μ=0.88cp,andBo=1.32bbl/STB. (a) Whatistheproductivityindexofthewell? (b) Whatistheaveragepermeabilityoftheformation? (c) Whatisthecapacityoftheformation? Problems 287 8.18 Aproducingformationconsistsoftwostrata:one15ftthickand150mdinpermeability,the other10ftthickand400mdinpermeability. (a) Whatistheaveragepermeability? (b) Whatisthecapacityoftheformation? (c) Ifduringawellworkover,the150mdstratumpermeabilityisreducedto25mdoutto aradiusof4ftandthe400mdstratumisreducedto40mdouttoan8ftradius,what istheaveragepermeabilityaftertheworkover,assumingnocrossflowbetweenbeds? Use re=500ftandrw=0.5ft. (d) Towhatpercentageoftheoriginalproductivityindexwillthewellbereduced? (e) Whatisthecapacityofthedamagedformation? 8.19 (a) P lotpressureversusradiusonbothlinearandsemilogpaperat0.1,1.0,10,and100 daysforpe=2500psia,q=300STB/day,Bo=1.32bbl/STB,μ=0.44cp,k=25md, h=43ft,ct=18×10–6 psi–1, and φ=0.16. (b) Assumingthatapressuredropof5psicanbeeasilydetectedwithapressuregauge, howlongmustthewellbeflowedtoproducethisdropinawelllocated1200ftaway? (c) Supposetheflowingwellislocated200ftdueeastofanorth-southfault.Whatpressuredropwilloccurafter10daysofflow,inashut-inwelllocated600ftduenorthof theflowingwell? (d) Whatwillthepressuredropbeinashut-inwell500ftfromtheflowingwellwhen theflowingwellhasbeenshutinforoneday,followingaflowperiodof5daysat300 STB/day? 8.20 Ashut-inwellislocated500ftfromonewelland1000ftfromasecondwell.Thefirstwell flowsfor3daysat250STB/day,atwhichtimethesecondwellbeginstoflowat400STB/day. Whatisthepressuredropintheshut-inwellwhenthesecondwellhasbeenflowingfor5days (i.e.,thefirsthasbeenflowingatotalof8days)?UsethereservoirconstantsofProblem8.19. 8.21 Awellisopenedtoflowat200STB/dayfor1day.Theseconddayitsflowisincreasedto 400STB/dayandthethirdto600STB/day.Whatisthepressuredropcausedinashut-in well500ftawayafterthethirdday?UsethereservoirconstantsofProblem8.19. 8.22 Thefollowingdatapertaintoavolumetricgasreservoir: Netformationthickness=15ft Hydrocarbonporosity=20% Initialreservoirpressure=6000psia Reservoirtemperature=190°F Gasviscosity=0.020cp Casingdiameter=6in. Averageformationpermeability=6md Chapter 8 288 • Single-Phase Fluid Flow in Reservoirs (a) Assumingidealgasbehavioranduniformpermeability,calculatethepercentageofrecoveryfroma640-acunitforaproducingrateof4.00MMSCF/daywhentheflowing wellpressurereaches500psia. (b) Iftheaveragereservoirpermeabilityhadbeen60mdinsteadof6md,whatrecovery wouldbeobtainedat4MMSCF/dayandaflowingwellpressureof500psia? (c) Recalculatepart(a)foraproductionrateof2MMSCF/day. (d) Supposefourwellsaredrilledonthe640-acunit,andeachisproducedat4.00MMSCF/ day.For6mdand500psiaminimumflowingwellpressure,calculatetherecovery. 8.23 Asandstonereservoir,producingwellaboveitsbubble-pointpressure,containsonlyone producingwell,whichisflowingonlyoilataconstantrateof175STB/day.Tenweeksafter thiswellbeganproducing,anotherwellwascompleted660ftawayinthesameformation. Onthebasisofthereservoirpropertiesthatfollow,estimatetheinitialformationpressure thatshouldbeencounteredbythesecondwellatthetimeofcompletion: φ=15% h=30ft co=18(10) psi –6 cw=3(10) psi –6 –1 cf=4.3(10) psi –6 μ=2.9cp –1 k=35md rw=0.33ft –1 Sw=33% pi=4300psia Bo=1.25bbl/STB 8.24 Develop an equation to calculate and then calculate the pressure at well 1, illustrated in Fig.8.24,ifthewellhasflowedfor5daysataflowrateof200STB/day: Fault 1 200' 300' Well 1 Fault 2 Figure 8.24 Problems 289 φ=25% h=20ft ct=30(10) psi –6 μ,=0.5cp –1 k=50md Bo=1.32bbl/STB rw=0.33ft pi=4000psia 8.25 Apressuredrawdowntestwasconductedonthediscoverywellinanewreservoirtoestimatethedrainagevolumeofthereservoir.Thewellwasflowedataconstantrateof125 STB/day.Thebottom-holepressuredata,aswellasotherrockandfluidpropertydata,follow.Whatarethedrainagevolumeofthewellandtheaveragepermeabilityofthedrainage volume?Theinitialreservoirpressurewas3900psia. Bo=1.1bbl/STB μo=0.80cp φ=20% h=22ft So=80% Sw=20% co=10(10) psi cw=3(10)–6 psi–1 cf =4(10)–6 psi–1 rw=0.33ft Time in hours pwf (psi) 0.5 3657 1.0 3639 1.5 3629 2.0 3620 3.0 3612 5.0 3598 7.0 3591 10.0 3583 20.0 3565 30.0 3551 40.0 3548 50.0 3544 60.0 3541 70.0 3537 80.0 3533 –6 –1 90.0 3529 100.0 3525 120.0 3518 150.0 3505 Chapter 8 290 • Single-Phase Fluid Flow in Reservoirs 8.26 Theinitialaveragereservoirpressureinthevicinityofanewwellwas4150psia.Apressuredrawdowntestwasconductedwhilethewellwasflowedataconstantoilflowrateof 550STB/day.Theoilhadaviscosityof3.3cpandaformationvolumefactorof1.55bbl/ STB.Otherdata,alongwiththebottom-holepressuredatarecordedduringthedrawdown test,follow.Assumethatwellborestorageconsiderationsmaybeneglected,anddetermine thefollowing: (a) Thepermeabilityoftheformationaroundthewell (b) Anydamagetothewell (c) Thedrainagevolumeofthereservoircommunicatingtothewell φ=34.3% h=93ft ct=1(10)–5 psi–1 rw=0.5ft Time in hours pwf (psi) 1 4025 2 4006 3 3999 4 3996 6 3993 8 3990 10 3989 20 3982 30 3979 40 3979 50 3978 60 3977 70 3976 80 3975 8.27 Thefirstoilwellinanewreservoirwasflowedataconstantflowrateof195STB/dayuntil acumulativevolumeof361STBhadbeenproduced.Afterthisproductionperiod,thewell wasshutinandthebottom-holepressuremonitoredforseveralhours.Theflowingpressure justasthewellwasbeingshutinwas1790psia.Forthedatathatfollow,calculatetheformationpermeabilityandtheinitialreservoirpressure. Problems 291 Bo=2.15bbl/STB μo=0.85cp φ=11.5% h=23ft ct=1(10)–5 psi–1 rw=0.33ft Δt in hours pws (psi) 0.5 2425 1.0 2880 2.0 3300 3.0 3315 4.0 3320 5.0 3324 6.0 3330 8.0 3337 10.0 3343 12.0 3347 14.0 3352 16.0 3353 18.0 3356 8.28 Awelllocatedinthecenterofseveralotherwellsinaconsolidatedsandstonereservoir waschosenforapressurebuilduptest.Thewellhadbeenputonproductionatthesame timeastheotherwellsandhadbeenproducedfor80hrataconstantoilflowrateof 375STB/day.Thewellsweredrilledon80-acspacing.Forthepressurebuildupdata and other rock and fluid property data that follow, estimate a value for the formation permeabilityanddetermineifthewellisdamaged.Theflowingpressureatshut-inwas 3470psia. Bo=1.31bbl/STB μo=0.87cp φ=25.3% h=22ft So=80% Sw=20% co=17(10) psi –6 cf=4(10)–6 psi–1 –1 cw=3(10)–6 psi–1 rw=0.33ft Chapter 8 292 • Single-Phase Fluid Flow in Reservoirs Δt in hours pws (psi) 0.114 3701 0.201 3705 0.432 3711 0.808 3715 2.051 3722 4.000 3726 8.000 3728 17.780 3730 References 1. W.T.CardwellJr.andR.L.Parsons,“AveragePermeabilitiesofHeterogeneousOilSands,” Trans.AlME(1945),160,34. 2. J.Law,“AStatisticalApproachtotheInterstitialHeterogeneityofSandReservoirs,”Trans. AlME(1948),174,165. 3. RobertC.EarlougherJr.,Advances in Well Test Analysis,Vol.5,SocietyofPetroleumEngineersofAlME,1977. 4. I.FattandD.H.Davis,“ReductioninPermeabilitywithOverburdenPressure,”Trans.AlME (1952),195,329. 5. RobertA.WattenbargerandH.J.RameyJr.,“GasWellTestingwithTurbulence,Damageand WellboreStorage,”Jour. of Petroleum Technology(Aug.1968),877–87. 6. R.Al-Hussainy,H.J.RameyJr.,andP.B.Crawford,“TheFlowofRealGasesthroughPorous Media,”Trans.AlME(1966),237,624. 7. D.G.Russell,J.H.Goodrich,G.E.Perry,andJ.F.Bruskotter,“MethodsforPredictingGas WellPerformance,”Jour. of Petroleum Technology(Jan.1966),99–108. 8. Theory and Practice of the Testing of Gas Wells, 3rd ed., Energy Resources Conservation Board,1975. 9. L.P.Dake,Fundamentals of Reservoir Engineering,Elsevier,1978. 10. C.S.MatthewsandD.G.Russell,Pressure Buildup and Flow Tests in Wells,Vol.1,Society ofPetroleumEngineersofAlME,1967. 11. R.Al-HussainyandH.J.RameyJr.,“ApplicationofRealGasFlowTheorytoWellTesting andDeliverabilityForecasting,”Jour. of Petroleum Technology(May1966),637–42;seealso Reprint Series, No. 9—Pressure Analysis Methods,SocietyofPetroleumEngineersofAlME, 1967,245–50. 12. A.F.vanEverdingenandW.Hurst,“TheApplicationoftheLaplaceTransformationtoFlow ProblemsinReservoirs,”Trans.AlME(1949),186,305–24. References 293 13. D. R. Horner, “Pressure Build-Up in Wells,” Proc. Third World Petroleum Congress, The Hague(1951),Sec.II,503–23;seealsoReprint Series, No. 9—Pressure Analysis Methods, SocietyofPetroleumEngineersofAlME,1967,25–43. 14. RoyalEugeneCollins,Flow of Fluids through Porous Materials,Reinhold,1961,108–23. 15. W.JohnLee,Well Testing,SocietyofPetroleumEngineers,1982. 16. A. F. van Everdingen, “The Skin Effect and Its Influence on the Productive Capacity of a Well,”Trans.AlME(1953),198,171. 17. W.Hurst,“EstablishmentoftheSkinEffectandItsImpedimenttoFluidFlowintoaWellbore,”Petroleum Engineering(Oct.1953),25, B-6. 18. D. R. Horner, “Pressure Build-Up in Wells,” Proc. Third World Petroleum Congress, The Hague(1951),Sec.II,503;seealsoReprint Series, No. 9—Pressure Analysis Methods,SocietyofPetroleumEngineersofAlME,1967,25. This page intentionally left blank C H A P T E R 9 Water Influx 9.1 Introduction Manyreservoirsareboundedonaportionoralloftheirperipheriesbywater-bearingrocks calledaquifers(fromLatin,aqua[water],ferre[tobear]).Theaquifersmaybesolarge(comparedwiththereservoirstheyadjoin)thattheyappearinfiniteforallpracticalpurposes;they mayalsobesosmallastobenegligibleintheireffectonreservoirperformance.Theaquifer itselfmaybeentirelyboundedbyimpermeablerocksothatthereservoirandaquifertogether formaclosed,orvolumetric,unit(Fig.9.1).Ontheotherhand,thereservoirmayoutcropat oneormoreplaceswhereitmaybereplenishedbysurfacewaters(Fig.9.2).Finally,anaquifermaybeessentiallyhorizontalwiththereservoiritadjoins,oritmayrise,asattheedgeof structural basins, considerably above the reservoir to provide some artesian kind of flow of watertothereservoir. Inresponsetoapressuredropinthereservoir,theaquiferreactstooffset,orretard,pressuredeclinebyprovidingasourceofwaterinfluxorencroachmentby(1)expansionofthewater, (2)expansionofotherknownorunknownhydrocarbonaccumulationsintheaquiferrock,(3)compressibilityoftheaquiferrock,and/or(4)artesianflow,whichoccurswhentheaquiferrisestoa levelabovethereservoir,whetheritoutcropsornot,andwhetherornottheoutcropisreplenished bysurfacewater. Todeterminetheeffectthatanaquiferhasontheproductionfromahydrocarbonreservoir, itisnecessarytobeabletocalculatetheamountofwaterthathasinfluxedintothereservoirfrom theaquifer.Thiscalculationcanbemadeusingthematerialbalanceequationwhentheinitialhydrocarbonamountandtheproductionareknown.TheHavlena-Odehapproachtomaterialbalance calculations,presentedinChapter3,cansometimesbeusedtoobtainanestimateforbothwater influxandinitialhydrocarbonamount.3,4Forthecaseofawater-drivereservoir,nooriginalgascap, andnegligiblecompressibilities,Eq.(3.13)reducestothefollowing: F = NEo+We 295 Chapter 9 296 • Water Influx E D C B A 50 + 34 + 1 0 0 34 50 + + 50 31 Andector + + 7 00 32 50 32 + + Wheeler + 00 33 TXL + 6 + 00 + 331150 + 3100 + 5 + + 0 305 + 4 Embar 00 32 + + + 0 25 +3 3 Martin 00 33 + + + 33 2 + + + + 50 33 8 0 5 10 Scale in miles Figure 9.1 A reservoir analyzer study of five fields, completed in a closed aquifer in the Ellenburger formation in West Texas (after Moore and Truby1). or F W =N+ e Eo Eo IfcorrectvaluesofWeareplacedinthisequationasafunctionofreservoirpressure,thenthe equationshouldplotasastraightlinewithintercept,N,andslopeequaltounity.TheproceduretosolveforbothWe and NinthiscaseinvolvesassumingamodelforWeasafunction ofpressure,calculatingWe,makingtheplotofF/EoversusWe/Eo,andobservingifastraight lineisobtained.Ifastraightlineisnotobtained,thenanewmodelforWeisassumedandthe procedurerepeated. 9.2 Steady-State Models 297 6000 6000 Surface water inlet 5000 Formation water discharge 4000 4000 3000 2000 1000 Sea level 1000 3000 + ++ + ++ + + + + + + + + + ++ + ++ ++ ++ ++ + Sheep ++ + ++ mtn. ++ ++ 20 Northwest Figure 9.2 5000 15 + + ++ ++ ++ ++ ++ + + ++ + + + ++ + + ++ ++ ++ Big + + + Horn +++ + mtn. ++ Torchlight dome 10 5 0 5 Distance from Torchlight, miles 10 15 2000 1000 Sea level 1000 20 East Geologic cross section through the Torchlight Tensleep Reservoir, Wyoming (after Stewart, Callaway, and Gladfelter2). Choosinganappropriatemodelforwaterinfluxinvolvesmanyuncertainties.Someofthese includethesizeandshapeoftheaquifer,andaquiferproperties,suchasporosityandpermeability. Normally,littleisknownabouttheseparameters,largelybecausethecosttodrillintotheaquifer toobtainthenecessarydataisnotoftenjustified. In this chapter, several models that have been used in reservoir studies to calculate water influxamountsareconsidered.Thesemodelscanbegenerallycategorizedbyatimedependence (i.e.,steadystateorunsteadystate)andwhethertheaquiferisanedgewaterorbottomwaterdrive. 9.2 Steady-State Models ThesimplestmodelthatwillbediscussedistheSchilthuissteady-statemodel,inwhichtherateof waterinflux,dWe/dt,isdirectlyproportionalto(pi – p),wherethepressure,p,ismeasuredattheoriginaloil-watercontact.5Thismodelassumesthatthepressureattheexternalboundaryoftheaquifer ismaintainedattheinitialvaluepiandthatflowtothereservoiris,byDarcy’slaw,proportionalto thepressuredifferential,assumingthewaterviscosity,averagepermeability,andaquifergeometry remainconstant: t We = k ' ∫ ( pi − p ) dt (9.1) dWe = k '( pi − p ) dt (9.2) 0 Chapter 9 298 • Water Influx wherek′isthewaterinfluxconstantinbarrelsperdayperpoundspersquareinchand(pi – p)isthe boundarypressuredropinpoundspersquareinch.Ifthevalueofk′canbefound,thenthevalueof thecumulativewaterinfluxWe canbefoundfromEq.(9.1)andaknowledgeofthepressurehistory ofthereservoir.If,duringanyreasonablylongperiod,therateofproductionandreservoirpressure remainsubstantiallyconstant,thenitisobviousthatthevolumetricwithdrawalrate,orreservoir voidage rate,mustequalthewaterinfluxrate: Rateofactive Rateof free Rateof water dWe = oilvolumetric + gas volumetric + volumetric dt voidage voidage voidage Intermsofsingle-phaseoilvolumefactors, dN p dN p dW p dWe Bg + Bw = Bo + ( R − Rso ) dt dt dt dt (9.3) wheredNp/dtisthedailyoilrateinSTB/dayand(R – Rso)dNp/dtisthedailyfreegasrateinSCF/ day.Thesolutiongas-oilratioRsoissubtractedfromthenet daily or currentgas-oilratioRbecause thesolutiongasRsoisaccountedforintheoilvolumefactorBooftheoilvoidageterm.Equation (9.3)maybeadjustedtousethetwo-phasevolumefactorbyaddingandsubtractingthetermRsoiBgdNp/dtandgroupingas dN p dN p dW p dWe = Bo + ( Rsoi − Rso ) Bg + ( R − Rsoi ) Bg + Bw dt dt dt dt andsince[Bo + (Rsoi – Rso)Bg]isthetwo-phasevolumefactorBt, dN p dN p dW p dWe + Bw = Bt + ( R − Rsoi ) Bg dt dt dt dt (9.4) WhendWe/dthasbeenobtainedintermsofthevoidageratesbyEqs.(9.3)and(9.4),theinflux constantk′maybefoundusingEq.(9.2).Althoughtheinfluxconstantcanbeobtainedinthismanneronlywhenthereservoirpressurestabilizes,onceithasbeenfound,itmaybeappliedtoboth stabilizedandchangingreservoirpressures. Figure 9.3 shows the pressure and production history of the Conroe Field, Texas, and Fig. 9.4 gives the gas and two-phase oil volume factors for the reservoir fluids. Between 33 and39monthsafterthestartofproduction,thereservoirpressurestabilizednear2090psigand theproductionratewassubstantiallyconstantat44,100STB/day,withaconstantgas-oilratio of 825 SCF/STB.Water production during the period was negligible. Example 9.1 shows the 9.2 Steady-State Models 299 2200 Average reservoir pressure at 4000 ft subsea 2100 500 1000 Gas-oil ratio 500 Production rate, M STB/day Cumulative production, MM STB 80 60 Daily production Current gas-oil ratio, SCF/STB Pressure. psig 2300 0 40 20 0 Cumulative production 0 Figure 9.3 1 2 Time, years 3 4 Reservoir pressure and production data, Conroe Field (after Schilthuis5). calculationofthewaterinfluxconstantk′fortheConroeFieldfromdataforthisperiodofstabilizedpressure.Ifthepressurestabilizesandthewithdrawalratesarenotreasonablyconstant, thewaterinfluxfortheperiodofstabilizedpressuremaybeobtainedfromthetotaloil,gas,and watervoidagesfortheperiod, ΔWe = Bt ΔNp+(ΔGp – RsoiΔNp)Bg + BwΔWp whereΔGp, ΔNp, and ΔWparethegas,oil,andwaterproducedduringtheperiodinsurfaceunits. TheinfluxconstantisobtainedbydividingΔWebytheproductofthedaysintheintervalandthe stabilizedpressuredrop(pi – ps): k' = ΔWe Δt ( pi − ps ) Chapter 9 300 7.4 • Two-phase oil volume factor, ft3 per STB 8.2 9.0 9.8 Water Influx 10.6 2200 Pressure, psig 2000 1800 1600 1400 1200 0.006 Figure 9.4 0.008 0.010 0.012 Gas volume factor, ft3 per SCF 0.014 Pressure volume relations for the Conroe Field oil and original complement of dissolved gas (after Schilthuis5). Example 9.1 Calculating the Water Influx Constant When Reservoir Pressure Stabilizes Given Thepressure-volume-temperature(PVT)datafortheConroeFieldinFig.9.4areasfollows: pi=2275psig ps=2090psig(stabilizedpressure) Bt=7.520ft3/STBat2090psig Bg=0.00693ft3/SCFat2090psig Rsoi=600SCF/STB(initialsolutiongas) R=825SCF/STB,fromproductiondata dNp/dt=44,100STB/day,fromproductiondata dWp/dt = 0 Solution At2090psigbyEq.(9.4),thedailyvoidagerateis dN p dN p dW p dWe = Bt + ( R − Rsoi ) Bg + Bw dt dt dt dt (9.4) 9.2 Steady-State Models 301 dV = 7.520 × 44, 100 + (825 − 600 )0.00693 × 44, 100 + 0 dt =401,000ft3/day Sincethismustequalthewaterinfluxrateatstabilizedpressureconditions,byEq.(9.2), dWe = k '( pi − p ) dt (9.2) dV dWe = = 401, 000 = k '(2275 − 2090 ) dt dt k′=2170ft3/day/psi Awaterinfluxconstantof2170ft3/day/psimeansthatifthereservoirpressuresuddenlydropsfrom aninitialpressureof2275psigto,say,2265psig(i.e.,Δp=10psi)andremainstherefor10days, duringthisperiod,thewaterinfluxwillbe ΔWe1=2170×10×10=217,000ft3 Ifattheendof10daysitdropsto,say,2255psig(i.e.,Δp=20psi)andremainstherefor20days, thewaterinfluxduringthissecondperiodwillbe ΔWe2=2170×20×20=868,000ft3 Thereisfourtimestheinfluxinthesecondperiodbecausetheinfluxratewastwiceasgreat(becausethepressuredropwastwiceasgreat)andbecausetheintervalwastwiceaslong.Thecumulativewaterinfluxattheendof30days,then,is 30 30 We = k ' ∫ ( pi − p ) dt = k ' ∑ ( pi − p )Δ t 0 0 =2170[(2275–2265)×10+(2275–2255)×20] =1,085,000ft3 t InFig.9.5, ∫ ( pi − p )dt representstheareabeneaththecurveofpressure drop,(pt – p), 0 plottedversustime,oritrepresentstheareaabovethecurveofpressureversustime.Theareasmay befoundbygraphicalintegration. OneoftheproblemsassociatedwiththeSchilthuissteady-statemodelisthatasthewater isdrainedfromtheaquifer,thedistancethatthewaterhastotraveltothereservoirincreases. Chapter 9 302 • Water Influx Pi B C Pressure drop Pressure A P1 P2 Pi – P3 Pi – P2 Pi – P1 P3 A 0 Figure 9.5 T1 T2 Time T3 0 B T1 T2 Time C T3 Plot of pressure and pressure drop versus time. Hurst suggested a modification to the Schilthuis equation by including a logarithmic term to accountforthisincreasingdistance.6TheHurstmethodhasmetwithlimitedapplicationandis infrequentlyused. We = c ' ∫ t 0 ( pi − p )dt log at dWe c '( pi − p ) = dt log at wherec′isthewaterinfluxconstantinbarrelsperdayperpoundspersquareinch,(pi – p)isthe boundarypressuredropinpoundspersquareinch,andaisatimeconversionconstantthatdepends ontheunitsofthetimet. 9.3 Unsteady-State Models Innearlyallapplications,thesteady-statemodelsdiscussedintheprevioussectionarenotadequateindescribingthewaterinflux.ThetransientnatureoftheaquiferssuggeststhatatimedependenttermbeincludedinthecalculationsforWe.Inthenexttwosections,unsteady-state modelsforbothedgewaterandbottomwaterdrivesarepresented.Anedgewaterdriveisonein whichthewaterinfluxentersthehydrocarbonbearingformationfromitsflankswithnegligible flowintheverticaldirection.Incontrast,abottomwaterdrivehassignificantverticalflow. 9.3 Unsteady-State Models 9.3.1 303 The van Everdingen and Hurst Edgewater Drive Model ConsideracircularreservoirofradiusrR,asshowninFig.9.6,inahorizontalcircularaquiferof radiusre,whichisuniforminthickness,permeability,porosity,andinrockandwatercompressibilities.Theradialdiffusivityequation,Eq.(8.35),expressestherelationshipbetweenpressure, radius,andtime,foraradialsystemsuchasFig.9.6,wherethedrivingpotentialofthesystemis thewaterexpandabilityandtherockcompressibility: ∂p ∂2 p 1 ∂p φ µct + = 2 r ∂r 0.0002637 k ∂t ∂r (8.35) ThisequationwassolvedinChapter8forwhatisreferredtoastheconstant terminal rate case.The constantterminalratecaserequiresaconstantflowrateattheinnerboundary,whichwasthewellboreforthesolutionsofChapter8.ThiswasappropriatefortheapplicationsofChapter8,since itwasdesiroustoknowthepressurebehavioratvariouspointsinthereservoirbecauseaconstant flowoffluidcameintothewellborefromthereservoir. re rR Figure 9.6 Circular reservoir inside a circular aquifer. Chapter 9 304 • Water Influx Inthischapter,thediffusivityequationisappliedtotheaquifer,wheretheinnerboundary isdefinedastheinterfacebetweenthereservoirandtheaquifer.Withtheinterfaceastheinner boundary,itwouldbemoreusefultorequirethepressureattheinnerboundarytoremainconstant andobservetheflowrateasitcrossestheboundaryorasitentersthereservoirfromtheaquifer. Mathematically,thisconditionisstatedas p=constant=pi – Δpatr = rR (9.5) whererRisaconstantandisequaltotheouterradiusofthereservoir(i.e.,theoriginaloil-water contact).Thepressurepmustbedeterminedatthisoriginaloil-watercontact.VanEverdingenand Hurst7solvedthediffusivityequationforthiscondition,whichisreferredtoastheconstant terminal pressure case,andthefollowinginitialandouterboundaryconditions: Theinitial condition is p = piforallvaluesofr Theouterboundaryconditionforaninfiniteaquiferis p = piatr = ∞ Theouterboundaryconditionforafiniteaquiferis ∂p = 0at r = re ∂r At this point, the diffusivity equation is rewritten in terms of the following dimensionless parameters: Dimensionlesstimeis tD=0.0002637 kt φ µct rR2 Dimensionlessradiusis rD = r rR Dimensionlesspressureis pD = pi − p pi − pwf (9.6) 9.3 Unsteady-State Models 305 wherek=averageaquiferpermeability,md;t=time,hours; φ=aquiferporosity,fraction; μ = waterviscosity,cp;ct=aquifercompressibility,psi–1;andrR=reservoirradius,feet.Withthese dimensionlessparameters,thediffusivityequationbecomes ∂2 pD 1 ∂pD ∂pD + = ∂t D rD ∂rD ∂rD2 (9.7) Van Everdingen and Hurst converted their solutions to dimensionless, cumulative water influx valuesandmadetheresultsavailableinaconvenientform,heregiveninTables9.1and9.2for variousratiosofaquifertoreservoirsize,expressedbytheratiooftheirradii,re/rR.Figures9.7to 9.10areplotsofsomeofthetabularvalues.Thedataaregivenintermsofdimensionlesstime, tD, anddimensionlesswaterinflux,WeD,sothatonesetofvaluessufficesforallaquiferswhose behaviorcanberepresentedbytheradialformofthediffusivityequation.Thewaterinfluxisthen foundbyusingEq.(9.8): We = B′ΔpWeD (9.8) where B ' = 1.119φ ct rR2 h θ 360 (9.9) B′isthewaterinfluxconstantinbarrelsperpoundspersquareinchandθistheanglesubtendedby thereservoircircumference(i.e.,forafullcircle,θ=360°,andforasemicircularreservoiragainst afault,θ=180°).ct is in psi–1 and rR and hareinfeet. Example9.2showstheuseofEq.(9.8)andthevaluesofTables9.1and9.2tocalculate the cumulative water influx at successive periods for the case of a constant reservoir boundary pressure.Theinfiniteaquifervaluesmaybeusedforsmalltimevalues,eventhoughtheaquiferis limitedinsize. Example 9.2 Calculating the Water Influx into a Reservoir Thisexampleshowshowtocalculatethewaterinfluxafter100days,200days,400days,and 800daysintoareservoir,theboundarypressureofwhichissuddenlyloweredandheldat2724 psia(pi=2734psia). Given φ=20% k=83md ct=8(10)–6 psi–1 rR=3000ft re=30,000ft μ=0.62cp Chapter 9 306 • Water Influx θ=360° h=40ft Solution FromEq.(9.6), tD=0.0002637 tD = kt φ µct rR2 0.0002637(83)t = 0.00245t 0.20(0.62 )[ 8(10 )−6 ]3000 2 FromEq.(9.9), B ' = 1.119φ ct rR2 h θ 360 (9.9) 360 =644.5 B′=1.119(0.20)[8(10)–6](30002)(40) 360 At100days,tD=0.00245(100)(24)=5.88dimensionlesstimeunits.Fromthere/rR=10curveof Fig.9.8,thevaluetD =5.88isusedtofindthecorrespondinginfluxofWeD=5.07dimensionless influxunits.ThissamevaluemayalsobefoundbyinterpolationofTable9.1,sincebelowtD=15, theaquiferbehavesessentiallyasifitwasinfinite,andnovaluesaregiveninTable9.2,sinceΔp = 2734–2724=10psiandwaterinfluxat100daysfromEq.(9.8)is We = B′ΔpWeD=644.5(10)(5.07)=32,680bbl Table 9.1 Infinite Aquifer Values of Dimensionless Water Influx WeD for Values of Dimensionless Time tD 307 Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD 0.00 0.000 79 35.697 455 150.249 1190 340.843 3250 816.090 35.000 6780.247 0.01 0.112 80 36.058 460 151.640 1200 343.308 3300 827.088 40.000 7650.096 0.05 0.278 81 36.418 465 153.029 1210 345.770 3350 838.067 50.000 9363.099 0.10 0.404 82 36.777 470 154.416 1220 348.230 3400 849.028 60.000 11,047.299 0.15 0.520 83 37.136 475 155.801 1225 349.460 3450 859.974 70.000 12,708.358 0.20 0.606 84 37.494 480 157.184 1230 350.688 3500 870.903 75.000 13,531.457 0.25 0.689 85 37.851 485 158.565 1240 353.144 3550 881.816 80.000 14,350.121 0.30 0.758 86 38.207 490 159.945 1250 355.597 3600 892.712 90.000 15,975.389 0.40 0.898 87 38.563 495 161.322 1260 358.048 3650 903.594 100.000 17,586.284 0.50 1.020 88 38.919 500 162.698 1270 360.496 3700 914.459 125.000 21,560.732 0.60 1.140 89 39.272 510 165.444 1275 361.720 3750 925.309 1.5(10) 2.538(10)4 0.70 1.251 90 39.626 520 168.183 1280 362.942 3800 936.144 2.0″ 3.308″ 5 0.80 1.359 91 39.979 525 169.549 1290 365.386 3850 946.966 2.5″ 4.066″ 0.90 1.469 92 40.331 530 170.914 1300 367.828 3900 957.773 3.0″ 4.817″ 1 1.569 93 40.684 540 173.639 1310 370.267 3950 968.566 4.0″ 6.267″ 2 2.447 94 41.034 550 176.357 1320 372.704 4000 979.344 5.0″ 7.699″ 3 3.202 95 41.385 560 179.069 1325 373.922 4050 990.108 6.0″ 9.113″ 4 3.893 96 41.735 570 181.774 1330 375.139 4100 1000.858 7.0″ 1.051(10)5 5 4.539 97 42.084 575 183.124 1340 377.572 4150 1011.595 8.0″ 1.189″ 6 5.153 98 42.433 589 184.473 1350 380.003 4200 1022.318 9.0″ 1.326″ 7 5.743 99 42.781 590 187.166 1360 382.432 4250 1033.028 1.0(10)6 1.462″ 8 6.314 100 43.129 600 189.852 1370 384.859 4300 1043.724 1.5″ 2.126″ 9 6.869 105 44.858 610 192.533 1375 386.070 4350 1054.409 2.0″ 2.781″ 10 7.411 110 46.574 620 195.208 1380 387.283 4400 1065.082 2.5″ 3.427″ (continued) Table 9.1 Infinite Aquifer Values of Dimensionless Water Influx WeD for Values of Dimensionless Time tD (continued) Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD 11 7.940 115 48.277 625 196.544 1390 389.705 4450 1075.743 3.0″ 4.064″ 12 8.457 120 49.968 630 197.878 1400 392.125 4500 1086.390 4.0″ 5.313″ 13 8.964 125 51.648 640 200.542 1410 394.543 4550 1097.024 5.0″ 6.544″ 14 9.461 130 53.317 650 203.201 1420 396.959 4600 1107.646 6.0″ 7.761″ 15 9.949 135 54.976 660 205.854 1425 398.167 4650 1118.257 7.0″ 8.965″ 16 10.434 140 56.625 670 208.502 1430 399.373 4700 1128.854 8.0″ 1.016″ 308 17 10.913 145 58.265 675 209.825 1440 401.786 4750 1139.439 9.0″ 1.134″ 18 11.386 150 59.895 680 211.145 1450 404.197 4800 1150.012 1.0(10)7 1.252″ 19 11.855 155 61.517 690 213.784 1460 406.606 4850 1160.574 1.5″ 1.828″ 20 12.319 160 63.131 700 216.417 1470 409.013 4900 1171.125 2.0″ 2.398″ 21 12.778 165 64.737 710 219.046 1475 410.214 4950 1181.666 2.5″ 2.961″ 22 13.233 170 66.336 720 221.670 1480 411.418 5000 1192.198 3.0″ 3.517″ 23 13.684 175 67.928 725 222.980 1490 413.820 5100 1213.222 4.0″ 4.610″ 24 14.131 180 69.512 730 224.289 1500 416.220 5200 1234.203 5.0″ 5.689″ 25 14.573 185 71.090 740 226.904 1525 422.214 5300 1255.141 6.0″ 6.758″ 26 15.013 190 72.661 750 229.514 1550 428.196 5400 1276.037 7.0″ 7.816″ 27 15.450 195 74.226 760 232.120 1575 434.168 5500 1296.893 8.0″ 8.866″ 28 15.883 200 75.785 770 234.721 1600 440.128 5600 1317.709 9.0″ 9.911″ 29 16.313 205 77.338 775 236.020 1625 446.077 5700 1338.486 1.0(10)8 1.095(10)7 30 16.742 210 78.886 780 237.318 1650 452.016 5800 1359.225 1.5″ 1.604″ 31 17.167 215 80.428 790 239.912 1675 457.945 5900 1379.927 2.0″ 2.108″ 32 17.590 220 81.965 800 242.501 1700 463.863 6000 1400.593 2.5″ 2.607″ 33 18.011 225 83.497 810 245.086 1725 469.771 6100 1421.224 3.0″ 3.100″ 34 18.429 230 85.023 820 247.668 1750 475.669 6200 1441.820 4.0″ 4.071″ Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD 35 18.845 235 86.545 825 248.957 1775 481.558 6300 1462.383 5.0″ 5.032″ 36 19.259 240 88.062 830 250.245 1800 487.437 6400 1482.912 6.0″ 5.984″ 37 19.671 245 89.575 840 252.819 1825 493.307 6500 1503.408 7.0″ 6.928″ 38 20.080 250 91.084 850 255.388 1850 499.167 6600 1523.872 8.0″ 7.865″ 39 20.488 255 92.589 860 257.953 1875 505.019 6700 1544.305 9.0″ 8.797″ 40 20.894 260 94.090 870 260.515 1900 510.861 6800 1564.706 1.0(10)9 9.725″ 41 21.298 265 95.588 875 261.795 1925 516.695 6900 1585.077 1.5″ 1.429(10)8 42 21.701 270 97.081 880 263.073 1950 522.520 7000 1605.418 2.0″ 1.880″ 43 22.101 275 98.571 890 265.629 1975 528.337 7100 1625.729 2.5″ 2.328″ 309 44 22.500 280 100.057 900 268.181 2000 534.145 7200 1646.011 3.0″ 2.771″ 45 22.897 285 101.540 910 270.729 2025 539.945 7300 1666.265 4.0″ 3.645″ 46 23.291 290 103.019 920 273.274 2050 545.737 7400 1686.490 5.0″ 4.510″ 47 23.684 295 104.495 925 274.545 2075 551.522 7500 1706.688 6.0″ 5.368″ 48 24.076 300 105.968 930 275.815 2100 557.299 7600 1726.859 7.0″ 6.220″ 49 24.466 305 107.437 940 278.353 2125 563.068 7700 1747.002 8.0″ 7.066″ 50 24.855 310 108.904 950 280.888 2150 568.830 7800 1767.120 9.0″ 51 25.244 315 110.367 960 283.420 2175 574.585 7900 1787.212 1.0(10) 8.747″ 52 25.633 320 111.827 970 285.948 2200 580.332 8000 1807.278 1.5″ 1.288(10)9 7.909″ 10 53 26.020 325 113.284 975 287.211 2225 586.072 8100 1827.319 2.0″ 1.697″ 54 26.406 330 114.738 980 288.473 2250 591.806 8200 1847.336 2.5″ 2.103″ 55 26.791 335 116.189 990 290.995 2275 597.532 8300 1867.329 3.0″ 2.505″ 56 27.174 340 117.638 1000 293.514 2300 603.252 8400 1887.298 4.0″ 3.299″ 57 27.555 345 119.083 1010 296.030 2325 608.965 8500 1907.243 5.0″ 4.087″ 4.868″ 58 27.935 350 120.526 1020 298.543 2350 614.672 8600 1927.166 6.0″ 59 28.314 355 121.966 1025 299.799 2375 620.372 8700 1947.065 7.0″ 5.643″ (continued) Table 9.1 Infinite Aquifer Values of Dimensionless Water Influx WeD for Values of Dimensionless Time tD (continued) Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD 60 28.691 360 123.403 1030 301.053 2400 626.066 8800 1966.942 8.0″ 6.414″ 61 29.068 365 124.838 1040 303.560 2425 631.755 8900 1986.796 9.0″ 7.183″ 62 29.443 370 126.720 1050 306.065 2450 637.437 9000 2006.628 1.0(10)11 7.948″ 63 29.818 375 127.699 1060 308.567 2475 643.113 9100 2026.438 1.5″ 1.17(10)″ 64 30.192 380 129.126 1070 311.066 2500 648.781 9200 2046.227 2.0″ 1.55″ 65 30.565 385 130.550 1075 312.314 2550 660.093 9300 2065.996 2.5″ 1.92″ 66 30.937 390 131.972 1080 313.562 2600 671.379 9400 2085.744 3.0″ 2.29″ 310 67 31.308 395 133.391 1090 316.055 2650 682.640 9500 2105.473 4.0″ 3.02″ 68 31.679 400 134.808 1100 318.545 2700 693.877 9600 2125.184 5.0″ 3.75″ 69 32.048 405 136.223 1110 321.032 2750 705.090 9700 2144.878 6.0″ 4.47″ 70 32.417 410 137.635 1120 323.517 2800 716.280 9800 2164.555 7.0″ 5.19″ 71 32.785 415 139.045 1125 324.760 2850 727.449 9900 2184.216 8.0″ 5.89″ 72 33.151 420 140.453 1130 326.000 2900 738.598 10,000 2203.861 9.0″ 6.58″ 73 33.517 425 141.859 1140 328.480 2950 749.725 12,500 2688.967 1.0(10)12 7.28″ 74 33.883 430 143.262 1150 330.958 3000 760.833 15,000 3164.780 1.5″ 1.08(10)11 75 34.247 435 144.664 1160 333.433 3050 771.922 17,500 3633.368 2.0″ 1.42″ 76 34.611 440 146.064 1170 335.906 3100 782.992 20,000 4095.800 77 34.974 445 147.461 1175 337.142 3150 794.042 25,000 5005.726 78 35.336 450 148.856 1180 338.376 3200 805.075 30,000 5899.508 Table 9.2 Limited Aquifer Values of Dimensionless Water Influx WeD for Values of Dimensionless Time tD and for Several Ratios of AquiferReservoir Radii re/rR re/rR = 1.5 re/rR = 2.0 re/rR = 2.5 re/rR = 3.0 Fluid influx, WeD re/rR = 3.5 Fluid influx, WeD re/rR = 4.0 Fluid influx, WeD re/rR = 4.5 Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD 5.0(10)–2 0.276 5.0(10)–2 0.278 1.0(10)–1 0.408 3.0(10)–1 0.755 1.00 1.571 2.00 2.442 2.5 2.835 6.0″ 0.304 7.5″ 0.345 1.5″ 0.509 4.0″ 0.895 1.20 1.761 2.20 2.598 3.0 3.196 7.0″ 0.330 1.0(10)–1 0.404 2.0″ 0.599 5.0″ 1.023 1.40 1.940 2.40 2.748 3.5 3.537 8.0″ 0.354 1.25″ 0.458 2.5″ 0.681 6.0″ 1.143 1.60 2.111 2.60 2.893 4.0 3.859 0.375 1.50″ 0.507 3.0″ 0.758 7.0″ 1.256 1.80 2.273 2.80 3.034 4.5 4.165 9.0″ 1.0(10) 1.1″ –1 Dimensionless time, tD Dimensionless time, tD Dimensionless time, tD 0.395 1.75″ 0.553 3.5″ 0.829 8.0″ 1.363 2.00 2.427 3.00 3.170 5.0 4.454 0.414 2.00″ 0.597 4.0″ 0.897 9.0″ 1.465 2.20 2.574 3.25 3.334 5.5 4.727 311 1.2″ 0.431 2.25″ 0.638 4.5″ 0.962 1.00 1.563 2.40 2.715 3.50 3.493 6.0 4.986 1.3″ 0.446 2.50″ 0.678 5.0″ 1.024 1.25 1.791 2.60 2.849 3.75 3.645 6.5 5.231 1.4″ 0.461 2.75″ 0.715 5.5″ 1.083 1.50 1.997 2.80 2.976 4.00 3.792 7.0 5.464 1.5″ 0.474 3.00″ 0.751 6.0″ 1.140 1.75 2.184 3.00 3.098 4.25 3.932 7.5 5.684 1.6″ 0.486 3.25″ 0.785 6.5″ 1.195 2.00 2.353 3.25 3.242 4.50 4.068 8.0 5.892 1.7″ 0.497 3.50″ 0.817 7.0″ 1.248 2.25 2.507 3.50 3.379 4.75 4.198 8.5 6.089 1.8″ 0.507 3.75″ 0.848 7.5″ 1.299 2.50 2.646 3.75 3.507 5.00 4.323 9.0 6.276 1.9″ 0.517 4.00″ 0.877 8.0″ 1.348 2.75 2.772 4.00 3.628 5.50 4.560 9.5 6.453 2.0″ 0.525 4.25″ 0.905 8.5″ 1.395 3.00 2.886 4.25 3.742 6.00 4.779 10 6.621 2.1″ 0.533 4.50″ 0.932 9.0″ 1.440 3.25 2.990 4.50 3.850 6.50 4.982 11 6.930 2.2″ 0.541 4.75″ 0.958 9.5″ 1.484 3.50 3.084 4.75 3.951 7.00 5.169 12 7.208 2.3″ 0.548 5.00″ 0.983 1.0 1.526 3.75 3.170 5.00 4.047 7.50 5.343 13 7.457 2.4″ 0.554 5.50″ 1.028 1.1 1.605 4.00 3.247 5.50 4.222 8.00 5.504 14 7.680 2.5″ 0.559 6.00″ 1.070 1.2 1.679 4.25 3.317 6.00 4.378 8.50 5.653 15 7.880 2.6″ 0.565 6.50″ 1.108 1.3 1.747 4.50 3.381 6.50 4.516 9.00 5.790 16 8.060 (continued) Table 9.2 Limited Aquifer Values of Dimensionless Water Influx WeD for Values of Dimensionless Time tD and for Several Ratios of AquiferReservoir Radii re/rR (continued) re/rR = 1.5 re/rR = 2.0 re/rR = 2.5 re/rR = 3.0 re/rR = 3.5 re/rR = 4.0 re/rR = 4.5 Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD Dimensionless time, tD Fluid influx, WeD 2.8″ 0.574 7.00″ 1.143 1.4 1.811 4.75 3.439 7.00 4.639 9.50 5.917 18 8.365 3.0″ 0.582 7.50″ 1.174 1.5 1.870 5.00 3.491 7.50 4.749 10 6.035 20 8.611 3.2″ 0.588 8.00″ 1.203 1.6 1.924 5.50 3.581 8.00 4.846 11 6.246 22 8.809 3.4″ 0.594 9.00″ 1.253 1.7 1.975 6.00 3.656 8.50 4.932 12 6.425 24 8.968 3.6″ 0.599 1.00″ 1.295 1.8 2.022 6.50 3.717 9.00 5.009 13 6.580 26 9.097 3.8″ 0.603 1.1 1.330 2.0 2.106 7.00 3.767 9.50 5.078 14 6.712 28 9.200 4.0″ 0.606 1.2 1.358 2.2 2.178 7.50 3.809 10.00 5.138 15 6.825 30 9.283 4.5″ 0.613 1.3 1.382 2.4 2.241 8.00 3.843 11 5.241 16 6.922 34 9.404 312 5.0″ 0.617 1.4 1.402 2.6 2.294 9.00 3.894 12 5.321 17 7.004 38 9.481 6.0″ 0.621 1.6 1.432 2.8 2.340 10.00 3.928 13 5.385 18 7.076 42 9.532 7.0″ 0.623 1.7 1.444 3.0 2.380 11.00 3.951 14 5.435 20 7.189 46 9.565 8.0″ 0.624 1.8 1.453 3.4 2.444 12.00 3.967 15 5.476 22 7.272 50 9.586 2.0 1.468 3.8 2.491 14.00 3.985 16 5.506 24 7.332 60 9.612 2.5 1.487 4.2 2.525 16.00 3.993 17 5.531 26 7.377 70 9.621 3.0 1.495 4.6 2.551 18.00 3.997 18 5.551 30 7.434 80 9.623 4.0 1.499 5.0 2.570 20.00 3.999 20 5.579 34 7.464 90 9.624 5.0 1.500 6.0 2.599 22.00 3.999 25 5.611 38 7.481 100 9.625 7.0 2.613 24.00 4.000 30 5.621 42 7.490 8.0 2.619 35 5.624 46 7.494 9.0 2.622 40 5.625 50 7.499 10.0 2.624 re/rR = 1.5 Dimensionless time, tD Fluid influx, WeD re/rR = 2.0 Dimensionless time, tD Fluid influx, WeD re/rR = 2.5 Dimensionless time, tD Fluid influx, WeD re/rR = 3.0 Dimensionless time, tD Fluid influx, WeD re/rR = 3.5 Dimensionless time, tD Fluid influx, WeD re/rR = 4.0 Dimensionless time, tD re/rR = 4.5 Fluid influx, WeD Dimensionless time, tD 3.0 3.195 6.0 5.148 9.00 6.861 9 6.861 10 7.417 15 9.965 3.5 3.542 6.5 5.440 9.50 7.127 10 7.398 15 9.945 20 12.32 4.0 3.875 7.0 5.724 10 7.389 11 7.920 20 12.26 22 13.22 4.5 4.193 7.5 6.002 11 7.902 12 8.431 22 13.13 24 14.95 5.0 4.499 8.0 6.273 12 8.397 13 8.930 24 13.98 26 14.95 5.5 4.792 8.5 6.537 13 8.876 14 9.418 26 14.79 28 15.78 6.0 5.074 9.0 6.795 14 9.341 15 9.895 26 15.59 30 16.59 313 6.5 5.345 9.5 7.047 15 9.791 16 10.361 30 16.35 32 17.38 7.0 5.605 10.0 7.293 16 10.23 17 10.82 32 17.10 34 18.16 7.5 5.854 10.5 7.533 17 10.65 18 11.26 34 17.82 36 18.91 8.0 6.094 11 7.767 18 11.06 19 11.70 36 18.52 38 19.65 8.5 6.325 12 8.220 19 11.46 20 12.13 38 19.19 40 20.37 9.0 6.547 13 8.651 20 11.85 22 12.95 40 19.85 42 21.07 9.5 6.760 14 9.063 22 12.58 24 13.74 42 20.48 44 21.76 10 6.965 15 9.456 24 13.27 26 14.50 44 21.09 46 22.42 11 7.350 16 9.829 26 13.92 28 15.23 46 21.69 48 23.07 12 7.706 17 10.19 28 14.53 30 15.92 48 22.26 50 23.71 13 8.035 18 10.53 30 15.11 34 17.22 50 22.82 52 24.33 14 8.339 19 10.85 35 16.39 38 18.41 52 23.36 54 24.94 15 8.620 20 11.16 40 17.49 40 18.97 54 23.89 56 25.53 16 8.879 22 11.74 45 18.43 45 20.26 56 24.39 58 26.11 18 9.338 24 12.26 50 19.24 50 21.42 58 24.88 60 26.67 20 9.731 25 12.50 60 20.51 55 22.46 60 25.36 65 28.02 Fluid influx, WeD (continued) Table 9.2 Limited Aquifer Values of Dimensionless Water Influx WeD for Values of Dimensionless Time tD and for Several Ratios of AquiferReservoir Radii re/rR (continued) re/rR = 1.5 Dimensionless time, tD Fluid influx, WeD re/rR = 2.0 Dimensionless time, tD Fluid influx, WeD re/rR = 2.5 Dimensionless time, tD Fluid influx, WeD re/rR = 3.0 Dimensionless time, tD Fluid influx, WeD re/rR = 3.5 Dimensionless time, tD Fluid influx, WeD re/rR = 4.0 Dimensionless time, tD re/rR = 4.5 Fluid influx, WeD Dimensionless time, tD 22 10.07 31 13.74 70 21.45 60 23.40 65 26.48 70 29.29 24 10.35 35 14.40 80 22.13 70 24.98 70 27.52 75 30.49 26 10.59 39 14.93 90 22.63 80 26.26 75 28.48 80 31.61 28 10.80 51 16.05 100 23.00 90 27.28 80 29.36 85 32.67 30 10.98 60 16.56 120 23.47 100 28.11 85 30.18 90 33.66 34 11.26 70 16.91 140 23.71 120 29.31 90 30.93 95 34.60 38 11.46 80 17.14 160 23.85 140 30.08 95 31.63 100 35.48 314 42 11.61 90 17.27 180 23.92 160 30.58 100 32.27 120 38.51 46 11.71 100 17.36 200 23.96 180 30.91 120 34.39 140 40.89 500 24.00 50 11.79 110 17.41 60 11.91 120 17.45 200 31.12 140 35.92 160 42.75 240 31.34 160 37.04 180 44.21 70 11.96 130 17.46 280 31.43 180 37.85 200 45.36 80 11.98 140 17.48 320 31.47 200 38.44 240 46.95 90 11.99 150 17.49 360 31.49 240 39.17 280 47.94 100 12.00 160 17.49 400 31.50 280 39.56 320 48.54 120 12.00 180 17.50 500 31.50 320 39.77 360 48.91 200 17.50 360 39.88 400 49.14 220 17.50 400 39.94 440 49.28 440 39.97 480 49.36 480 39.98 Fluid influx, WeD 9.3 Unsteady-State Models 315 8 re /rR = ∞ re /rR = 4.0 7 Fluid influx, WeD 6 re /rR = 3.5 5 re /rR = 3.0 4 3 re /rR = 2.5 2 re /rR = 2.0 1 0.1 1 10 100 Dimensionless time, tD Figure 9.7 Limited aquifer values of dimensionless influx WeD for values of dimensionless time tD and aquifer limits given by the ratio re/rR. 7.4 Two-phase oil volume factor, ft3 per STB 8.2 9.0 9.8 10.6 2200 Pressure, psig 2000 1800 1600 1400 1200 0.006 Figure 9.8 0.008 0.010 0.012 Gas volume factor, ft3 per SCF 0.014 Limited aquifer values of dimensionless influx WeD for values of dimensionless time tD and aquifer limits given by the ratio re/rR. Chapter 9 316 70 • Water Influx re /rR = ∞ 60 re /rR = 10 Fluid influx, WeD 50 re /rR = 9 40 re /rR = 8 30 re /rR = 7 re /rR = 6 20 re /rR = 5 10 0 1 10 100 1000 Dimensionless time, tD Figure 9.9 Infinite aquifer values of dimensionless influx WeD for values of dimensionless time tD. Similarly,at t=100days tD=5.88 200days 400days 800days 11.76 23.52 47.04 WeD=5.07 8.43 13.90 22.75 We=32,680 54,330 89,590 146,600 Foraquifers99timesaslargeasthereservoirstheysurround,orre/rR=10,thismeansthatthe effectoftheaquiferlimitsarenegligiblefordimensionlesstimevaluesunder15andthatitissome timebeforetheaquiferlimitsaffectthewaterinfluxappreciably.ThisisalsoillustratedbythecoincidenceofthecurvesofFigs.9.7and9.8withtheinfiniteaquifercurveforthesmallertimevalues. Itshouldalsobenotedthat,unlikeasteady-statesystem,thevaluesofwaterinfluxcalculatedin Example9.2failtodoublewhenthetimeisdoubled. Whilewaterisenteringthereservoirfromtheaquiferatadecliningrate,inresponsetothe firstpressuresignalΔp1 = pi – p1,letasecond,suddenpressuredropΔp2 = p1 – p2(notpi – p2)be imposedatthereservoirboundaryatatimet1.Thisisanapplicationoftheprincipleofsuperposition,whichwasdiscussedinChapter8.Thetotalorneteffectisthesumofthetwo,asillustrated inFig.9.11,where,forsimplicity,Δp1 = Δp2 and t2=2t1.Theupperandmiddlecurvesrepresent 9.3 Unsteady-State Models 317 108 109 1010 106 103 107 104 Fluid influx, WeD 108 105 109 106 107 104 105 106 Dimesionless time, tD 107 Figure 9.10 Infinite aquifer values of dimensionless influx WeD for values of dimensionless time tD. pi t2 = 2 t1 = 1 Pressure ∆p1 p1 ∆p2 p2 rR Distance from reservoir boundary re Figure 9.11 Pressure distributions in an aquifer, due to two equal pressure decrements imposed at equal time intervals. Chapter 9 318 • Water Influx thepressuredistributionintheaquiferinresponsetothefirstsignalalone,attimest1 and t2, respectively.Theuppercurvemayalsobeusedtorepresentthepressuredistributionforthesecond pressuresignalaloneattimet2because,inthissimplifiedcase,Δp1 = Δp2 and Δt2 = Δt1.Thelower curve,then,isthesumoftheupperandmiddlecurves.Mathematically,thismeansthatEq.(9.10) canbeusedtocalculatethecumulativewaterinflux: We = B′ΣΔpWeD (9.10) ThiscalculationisillustratedinExample9.3. Example 9.3 Calculating the Water Influx When Reservoir Boundary Pressure Drops SupposeinExample9.2,attheendof100days,thereservoirboundarypressuresuddenlydrops top2=2704psia(i.e.,Δp2 = p1 – p2=20psi,not pi – p2=30psi).Calculatethewaterinfluxat400 daystotaltime. Given φ=20% k=83md ct=8(10)–6 psi–1 rR=3000ft re=30,000ft μ=0.62cp θ=360° h=40ft Solution ThewaterinfluxduetothefirstpressuredropΔp1=10psiat400dayswascalculatedinExample 9.2tobe89,590bbl.Thiswillbethesame,eventhoughasecondpressuredropoccursat100days andcontinuesto400days.Thisseconddropwillhaveactedfor300daysoradimensionlesstime oftD=0.0588×300=17.6.FromFig.9.8orTable9.2,re/rR=10andWeD=11.14fortD=17.6, andthewaterinfluxis ΔWe2 = B′ × Δp2 × WeD2 =644.5×20×11.14=143,600bbl We2 = ΔWe1 + ΔWe2 = B′ × Δp1 × WeD1 + B′ × Δp2 × WeD2 = B′ΣΔ pWeD =644.5(10×13.90+20×11.14) =89,590+143,600=233,190bbl 9.3 Unsteady-State Models Pi ∆P1 = ½(Pi – P1) P1 Average boundary pressure 319 ∆P2 = ½(Pi – P2) ∆P2 P2 ∆P3 ∆P3 = ½(P1 – P3) P3 ∆P4 = ½(P2 – P4) ∆P4 ∆P5 P4 0 1 2 3 4 5 Time periods Figure 9.12 Sketch showing the use of step pressures to approximate the pressure-time curve. Example9.3illustratesthecalculationofwaterinfluxwhenasecondpressuredropoccurs 100daysafterthefirstdropinExample9.2.Acontinuationofthismethodmaybeusedtocalculate thewaterinfluxintoreservoirsforwhichboundarypressurehistoriesareknownandalsoforwhich sufficientinformationisknownabouttheaquifertocalculatetheconstantB′andthedimensionless timetD. Thehistoryofthereservoirboundarypressuremaybeapproximatedascloselyasdesired byaseriesofstep-by-steppressurereductions(orincreases),asillustratedinFig.9.12.Thebest approximationofthepressurehistoryismadeasshownbymakingthepressurestepatanytime equaltohalfofthedropinthepreviousintervaloftimeplushalfofthedropinthesucceedingperiodoftime.8Whenreservoirboundarypressuresarenotknown,averagereservoirpressuresmay besubstitutedwithsomereductionintheaccuracyoftheresults.Inaddition,forbestaccuracy, theaverageboundarypressureshouldalwaysbethatattheinitialratherthanthecurrentoil-water contact;otherwise,amongotherchanges,adecreasingvalueofrRisunaccountedfor.Example9.4 illustratesthecalculationofwaterinfluxattwosuccessivetimevaluesforthereservoirshownin Fig.9.13. Example 9.4 Calculating the Water Influx for the Reservoir in Figure 9.13 Calculate the water influx at the third- and fourth-quarter years of production for the reservoir showninFig.9.13. Chapter 9 320 • Water Influx Given φ=20.9% k=275md(averagereservoirpermeability,presumedthesamefortheaquifer) μ=0.25cp ct = 6 ×10–6 psi–1 h=19.2ft;areaofreservoir=1216ac Estimatedareaofaquifer=250,000ac θ=180° Solution 1 Sincethereservoirisagainstafault A = π rR2 and 2 rR2 = 1216 × 43, 560 0.5 × 3.1416 rR = 5807ft fort=91.3days(one-quarteryearoroneperiod), tD=0.0002637 kt (275 )(91.3)(24 ) t = 0.0002637 = 15.0 2 D φ µct rR (0.209 )(0.25 )(6 × 10 −6 )(5807 )2 B ' = 1.119φ ct rR2 h θ 360 B′=1.119×0.209× 6 ×10–6 ×(5807)2 ×19.2×(180°/360°) =455bbl/psi N ult Fa 5810 ft 1216 acres Oi l- w t a t e r c o n t ac Figure 9.13 Sketch showing the equivalent radius of a reservoir. (9.9) 9.3 Unsteady-State Models 321 Table 9.3 Boundary Step Pressures and WeD Values for Example 9.4 Time period, t a Time in days, t Dimensionless time, tD Dimensionless influx, WeDa Average reservoir pressure, p (psia) Average boundary pressure, pB (psia) Step pressure, Δp (psi) 0 0 0 0.0 3793 3793 0.0 1 91.3 15 10.0 3786 3788 2.5 2 182.6 30 16.7 3768 3774 9.5 3 273.9 45 22.9 3739 3748 20.0 4 365.2 60 28.7 3699 3709 32.5 5 456.5 75 34.3 3657 3680 34.0 6 547.8 90 39.6 3613 3643 33.0 InfiniteaquifervaluesfromFig.9.9orTable9.1. Sincetheaquiferis250,000/1216=206timestheareaofthereservoir,foraconsiderable time,theinfiniteaquifervaluesmaybeused.Table9.3showsthevaluesofboundarysteppressures andtheWeDvaluesforthefirstsixperiods.ThecalculationofthesteppressuresΔpisillustratedin Fig.9.12.Forexample, Δp3=1/2(p1 – p3)=1/2(3788–3748)=20.0psi Tables9.4and9.5showthecalculationofΣΔp × WeDattheendofthethirdandfourthperiods, thevaluesbeing416.0and948.0,respectively.Thenthecorrespondingwaterinfluxattheendof theseperiodsis Table 9.4 Water Influx at the End of the Third Quarter for Example 9.4 tD WeD Δp Δp × WeD 45 22.9 2.5 57.3 30 16.7 9.5 158.7 15 10.0 20.0 200.0 Table 9.5 Water Influx at the End of the Fourth Quarter for Example 9.4 tD WeD Δp Δp × WeD 60 28.7 2.5 71.8 45 22.9 9.5 217.6 30 16.7 20.0 334.0 15 10.0 32.5 325.0 322 Chapter 9 • Water Influx We(3rdquarter)=B′ ΣΔp × WeD=455×416.0=189,300bbl We(4thquarter)=B′ ΣΔp × WeD=455×948.4=431,500bbl IncalculatingthewaterinfluxinExample9.4attheendofthethirdquarter,itshouldbe carefullynotedinTable9.4that,sincethefirstpressuredrop,Δp1=2.5psi,hadbeenoperatingfor thefullthreequarters(tD=45),itwasmultipliedbyWeD=22.9,whichcorrespondstotD=45.Similarly,forthefourth-quartercalculationinTable9.5,the2.5psiwasmultipliedbyWeD=28.7,which isthevaluefortD=60.ThustheWeDvaluesareinvertedsothattheonecorrespondingtothelongest timeismultipliedbythefirstpressuredropandviceversa.Also,incalculatingeachsuccessivevalueofΣΔp × WeD,itisnotsimplyamatterofaddinganewΔp × WeDtermtotheformersummation butacompleterecalculation,asshowninTables9.4and9.5.Considercontinuingthecalculations ofTable9.4and9.5forsuccessivequarters.Correctcalculationswillshowthatthewaterinflux valuesattheendofthefifthandsixthquartersare773,100and1,201,600bbl,respectively. From the previous discussion, it is evident that it is possible to calculate water influx independently of material balance calculations from a knowledge of the history of the reservoir, boundary pressure, and the dimensions and physical characteristics of the aquifer, as shown by Chatas.9Althoughstrictlyspeaking,thevanEverdingenandHurstsolutionstothediffusivityequationapplyonlytocircularreservoirssurroundedconcentricallybyhorizontal,circular(orinfinite) aquifersofconstantthickness,porosity,permeability,andeffectivewatercompressibility,formany engineeringpurposes,goodresultsmaybeobtainedwhenthesituationissomewhatlessthanideal, asitnearlyalwaysis.Theradiusofthereservoirmaybeapproximatedbyusingtheradiusofa circle,equalinareatotheareaofthereservoir,andwheretheapproximatesizeoftheaquiferis known,thesameapproximationmaybeusedfortheaquiferradius.Wheretheaquiferismorethan approximately99timesthesize(volume)ofthereservoir(re/rR=10),theaquiferbehavesessentiallyasifitwereinfiniteforaconsiderableperiod,sothatthevaluesofTable9.1maybeused.There are,tobesure,uncertaintiesinthepermeability,porosity,andthicknessoftheaquiferthatmustbe estimatedfrominformationobtainedfromwellsdrilledinthereservoirandwhateverwells,ifany, drilledintheaquifer.Theviscosityofthewatercanbeestimatedfromthetemperatureandpressure (Chapter2,section2.5.4),andthewaterandrockcompressibilitiescanbeestimatedfromthedata giveninChapter2,sections2.5.3and2.2.2. Becauseofthemanyuncertaintiesinthedimensionsandpropertiesoftheaquifer,thecalculationofwaterinfluxindependentlyofmaterialbalanceappearssomewhatunreliable.Forinstance, inExample9.4,itwasassumedthatthefaultagainstwhichthereservoiraccumulatedwasoflarge (actuallyinfinite)extent,andsincethepermeabilityofonlythereservoirrockwasknown,itwas assumedthattheaveragepermeabilityoftheaquiferwasalso275md.Theremaybevariationsinthe aquiferthicknessandporosity,andtheaquifermaycontainfaults,impermeableareas,andunknown hydrocarbonaccumulations—allofwhichcanintroducevariationsofgreaterorlesserimportance. AsExamples9.2,9.3,and9.4suggest,thecalculationsforwaterinfluxcanbecomelongand tedious.Theuseofthecomputerwiththesecalculationsrequireslargedatafilescontainingthe 9.3 Unsteady-State Models 323 valuesofWeD, tD, and re/rRfromTables9.1and9.2,aswellasatablelookuproutine.Severalauthorshaveattemptedtodevelopequationstodescribethedimensionlesswaterinfluxasafunction ofthedimensionlesstimeandradiusratio.10,11,12Theseequationsreducethedatastoragerequired whenusingthecomputerincalculationsofwaterinflux. In1960,CarterandTracydevelopedanapproximatemethodthatdoesnotusetheprinciple ofsuperposition.13Severalauthorshavedescribedthismodelbuthavepointedoutthat,whilesimplifyingthecalculations,theremaybealossofaccuracyincalculatingthewaterinflux.14–16The readerisencouragedtolookupthereferencesifthereisfurtherinterest. 9.3.2 Bottomwater Drive ThevanEverdingenandHurstmodeldiscussedintheprevioussectionisbasedontheradialdiffusivityequationwrittenwithoutatermdescribingverticalflowfromtheaquifer.Intheory,this modelshouldnotbeusedwhenthereissignificantmovementofwaterintothereservoirfroma bottomwaterdrive.Toaccountfortheflowofwaterinaverticaldirection,Coatsand,later,Allard andChenaddedatermtoEq.(9.35)toyieldthefollowing: ∂2 p ∂p ∂2 p 1 ∂p φ µct + + F = k 2 2 0.0002637 k ∂t r ∂r ∂r ∂z (9.10) whereFkistheratioofverticaltohorizontalpermeability.17,18 Usingthedefinitionsofdimensionlesstime,radius,andpressureandintroducingasecond dimensionlessdistance,zD,Eq.(9.10)becomesEq.(9.11): z= z rR Fk1/2 ∂2 p D 1 ∂ p D ∂2 p D ∂ p D + 2 = + ∂t D ∂z D ∂rD2 rD ∂ D (9.11) CoatssolvedEq.(9.11)fortheterminalratecaseforinfiniteaquifers.17AllardandChenusedanumericalsimulatortosolvetheproblemfortheterminalpressurecase.18Theydefinedawaterinflux constant,B′,andadimensionlesswaterinflux,WeD,analogoustothosedefinedbyvanEverdingen andHurst,exceptthatB′doesnotincludetheangleθ: B′=1.119φhct rR2 (9.12) The actual values of WeD will be different from those of the van Everdingen and Hurst model, becauseWeDforthebottomwaterdriveisafunctionoftheverticalpermeability.Becauseofthis functionality,thesolutionspresentedbyAllardandChen,foundinTables9.6to9.10,arefunctions oftwodimensionlessparameters, rD′ and zD′ : Chapter 9 324 Water Influx re rR (9.13) h rR Fk1/2 (9.14) rD′ = zD′ = • Themethodofcalculatingwaterinfluxfromthedimensionlessvaluesobtainedfromthesetables followsexactlythemethodillustratedinExamples9.2to9.4.TheprocedureisshowninExample 9.5,whichisaproblemtakenfromAllardandChen.18 Example 9.5 Calculating the Water Influx as a Function of Time Given rR=2000ft re = ∝ h=200ft k=50md Fk=0.04 φ=10% μ=0.395cp ct=8×10–6 psi–1 Time in days, t Average boundary pressure, pB (psia) 0 3000 30 2956 60 2917 90 2877 120 2844 150 2811 180 2791 210 2773 240 2755 Solution rD′ = ∞ zD′ = h rR Fk1/2 (9.14) 9.3 Unsteady-State Models 325 zD′ = 200 = 0.5 2000(0.040 )1/2 t D = 0.0002637 tD = kt φ µct rR2 0.0002637(50 )t = 0.0104 t (where t isinhours) 0.10(0.395 )8(10 )−6 2000 2 B ′ = 1.119φ hct rR2 (9.12) B′=1.119(0.10)(200)8(10)–620002=716bbl/psi Time in days, t Dimensionless Dimensionless influx, WeD time, tD Average boundary pressure, pB (psia) Step pressure, Δp Water influx, We (M bbl) 0 0 0 3000 0 0 30 7.5 5.038 2956 22.0 79 60 15.0 8.389 2917 41.5 282 90 22.5 11.414 2877 39.5 572 120 30.0 14.263 2844 36.5 933 150 37.5 16.994 2811 33.0 1353 180 45.0 19.641 2791 26.5 1810 210 52.5 22.214 2773 19.0 2284 240 60.0 24.728 2755 18.0 2782 Table 9.6 Dimensionless Influx, WeD, for Infinite Aquifer for Bottomwater Drive z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 0.1 0.700 0.677 0.508 0.349 0.251 0.195 0.176 0.2 0.793 0.786 0.696 0.547 0.416 0.328 0.295 0.3 0.936 0.926 0.834 0.692 0.548 0.440 0.396 0.4 1.051 1.041 0.952 0.812 0.662 0.540 0.486 0.5 1.158 1.155 1.059 0.918 0.764 0.631 0.569 0.6 1.270 1.268 1.167 1.021 0.862 0.721 0.651 0.7 1.384 1.380 1.270 1.116 0.953 0.806 0.729 0.8 1.503 1.499 1.373 1.205 1.039 0.886 0.803 0.9 1.621 1.612 1.477 1.286 1.117 0.959 0.872 (continued) Table 9.6 Dimensionless Influx, WeD, for Infinite Aquifer for Bottomwater Drive (continued) z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 1 1.743 1.726 1.581 1.347 1.181 1.020 0.932 2 2.402 2.393 2.288 2.034 1.827 1.622 1.509 3 3.031 3.018 2.895 2.650 2.408 2.164 2.026 4 3.629 3.615 3.477 3.223 2.949 2.669 2.510 5 4.217 4.201 4.048 3.766 3.462 3.150 2.971 6 4.784 4.766 4.601 4.288 3.956 3.614 3.416 7 5.323 5.303 5.128 4.792 4.434 4.063 3.847 8 5.829 5.808 5.625 5.283 4.900 4.501 4.268 9 6.306 6.283 6.094 5.762 5.355 4.929 4.680 10 6.837 6.816 6.583 6.214 5.792 5.344 5.080 11 7.263 7.242 7.040 6.664 6.217 5.745 5.468 12 7.742 7.718 7.495 7.104 6.638 6.143 5.852 13 8.196 8.172 7.943 7.539 7.052 6.536 6.231 14 8.648 8.623 8.385 7.967 7.461 6.923 6.604 15 9.094 9.068 8.821 8.389 7.864 7.305 6.973 16 9.534 9.507 9.253 8.806 8.262 7.682 7.338 17 9.969 9.942 9.679 9.218 8.656 8.056 7.699 18 10.399 10.371 10.100 9.626 9.046 8.426 8.057 19 10.823 10.794 10.516 10.029 9.432 8.793 8.411 20 11.241 11.211 10.929 10.430 9.815 9.156 8.763 21 11.664 11.633 11.339 10.826 10.194 9.516 9.111 22 12.075 12.045 11.744 11.219 10.571 9.874 9.457 23 12.486 12.454 12.147 11.609 10.944 10.229 9.801 24 12.893 12.861 12.546 11.996 11.315 10.581 10.142 25 13.297 13.264 12.942 12.380 11.683 10.931 10.481 26 13.698 13.665 13.336 12.761 12.048 11.279 10.817 27 14.097 14.062 13.726 13.140 12.411 11.625 11.152 28 14.493 14.458 14.115 13.517 12.772 11.968 11.485 29 14.886 14.850 14.501 13.891 13.131 12.310 11.816 30 15.277 15.241 14.884 14.263 13.488 12.650 12.145 31 15.666 15.628 15.266 14.634 13.843 12.990 12.473 32 16.053 16.015 15.645 15.002 14.196 13.324 12.799 33 16.437 16.398 16.023 15.368 14.548 13.659 13.123 34 16.819 16.780 16.398 15.732 14.897 13.992 13.446 326 z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 35 17.200 17.160 16.772 16.095 15.245 14.324 13.767 36 17.579 17.538 17.143 16.456 15.592 14.654 14.088 37 17.956 17.915 17.513 16.815 15.937 14.983 14.406 38 18.331 18.289 17.882 17.173 16.280 15.311 14.724 39 18.704 18.662 18.249 17.529 16.622 15.637 15.040 40 19.088 19.045 18.620 17.886 16.964 15.963 15.356 41 19.450 19.407 18.982 18.240 17.305 16.288 15.671 42 19.821 19.777 19.344 18.592 17.644 16.611 15.985 43 20.188 20.144 19.706 18.943 17.981 16.933 16.297 44 20.555 20.510 20.065 19.293 18.317 17.253 16.608 45 20.920 20.874 20.424 19.641 18.651 17.573 16.918 46 21.283 21.237 20.781 19.988 18.985 17.891 17.227 47 21.645 21.598 21.137 20.333 19.317 18.208 17.535 48 22.006 21.958 21.491 20.678 19.648 18.524 17.841 49 22.365 22.317 21.844 21.021 19.978 18.840 18.147 50 22.722 22.674 22.196 21.363 20.307 19.154 18.452 51 23.081 23.032 22.547 21.704 20.635 19.467 18.757 52 23.436 23.387 22.897 22.044 20.962 19.779 19.060 53 23.791 23.741 23.245 22.383 21.288 20.091 19.362 54 24.145 24.094 23.593 22.721 21.613 20.401 19.664 55 24.498 24.446 23.939 23.058 21.937 20.711 19.965 56 24.849 24.797 24.285 23.393 22.260 21.020 20.265 57 25.200 25.147 24.629 23.728 22.583 21.328 20.564 58 25.549 25.496 24.973 24.062 22.904 21.636 20.862 59 25.898 25.844 25.315 24.395 23.225 21.942 21.160 60 26.246 26.191 25.657 24.728 23.545 22.248 21.457 61 26.592 26.537 25.998 25.059 23.864 22.553 21.754 62 26.938 26.883 26.337 25.390 24.182 22.857 22.049 63 27.283 27.227 26.676 25.719 24.499 23.161 22.344 64 27.627 27.570 27.015 26.048 24.816 23.464 22.639 65 27.970 27.913 27.352 26.376 25.132 23.766 22.932 66 28.312 28.255 27.688 26.704 25.447 24.068 23.225 67 28.653 28.596 28.024 27.030 25.762 24.369 23.518 68 28.994 28.936 28.359 27.356 26.075 24.669 23.810 69 29.334 29.275 28.693 27.681 26.389 24.969 24.101 (continued) 327 Table 9.6 Dimensionless Influx, WeD, for Infinite Aquifer for Bottomwater Drive (continued) z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 70 29.673 29.614 29.026 28.006 26.701 25.268 24.391 71 30.011 29.951 29.359 28.329 27.013 25.566 24.681 72 30.349 30.288 29.691 28.652 27.324 25.864 24.971 73 30.686 30.625 30.022 28.974 27.634 26.161 25.260 74 31.022 30.960 30.353 29.296 27.944 26.458 25.548 75 31.357 31.295 30.682 29.617 28.254 26.754 25.836 76 31.692 31.629 31.012 29.937 28.562 27.049 26.124 77 32.026 31.963 31.340 30.257 28.870 27.344 26.410 78 32.359 32.296 31.668 30.576 29.178 27.639 26.697 79 32.692 32.628 31.995 30.895 29.485 27.933 26.983 80 33.024 32.959 32.322 31.212 29.791 28.226 27.268 81 33.355 33.290 32.647 31.530 30.097 28.519 27.553 82 33.686 33.621 32.973 31.846 30.402 28.812 27.837 83 34.016 33.950 33.297 32.163 30.707 29.104 28.121 84 34.345 34.279 33.622 32.478 31.011 29.395 28.404 85 34.674 34.608 33.945 32.793 31.315 29.686 28.687 86 35.003 34.935 34.268 33.107 31.618 29.976 28.970 87 35.330 35.263 34.590 33.421 31.921 30.266 29.252 88 35.657 35.589 34.912 33.735 32.223 30.556 29.534 89 35.984 35.915 35.233 34.048 32.525 30.845 29.815 90 36.310 36.241 35.554 34.360 32.826 31.134 30.096 91 36.636 36.566 35.874 34.672 33.127 31.422 30.376 92 36.960 36.890 36.194 34.983 33.427 31.710 30.656 93 37.285 37.214 36.513 35.294 33.727 31.997 30.935 94 37.609 37.538 36.832 35.604 34.026 32.284 31.215 95 37.932 37.861 37.150 35.914 34.325 32.570 31.493 96 38.255 38.183 37.467 36.233 34.623 32.857 31.772 97 38.577 38.505 37.785 36.532 34.921 33.142 32.050 98 38.899 38.826 38.101 36.841 35.219 33.427 32.327 99 39.220 39.147 38.417 37.149 35.516 33.712 32.605 100 39.541 39.467 38.733 37.456 35.813 33.997 32.881 105 41.138 41.062 40.305 38.987 37.290 35.414 34.260 110 42.724 42.645 41.865 40.508 38.758 36.821 35.630 115 44.299 44.218 43.415 42.018 40.216 38.221 36.993 328 z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 120 45.864 45.781 44.956 43.520 41.666 39.612 38.347 125 47.420 47.334 46.487 45.012 43.107 40.995 39.694 130 48.966 48.879 48.009 46.497 44.541 42.372 41.035 135 50.504 50.414 49.523 47.973 45.967 43.741 42.368 140 52.033 51.942 51.029 49.441 47.386 45.104 43.696 145 53.555 53.462 52.528 50.903 48.798 46.460 45.017 150 55.070 54.974 54.019 52.357 50.204 47.810 46.333 155 56.577 56.479 55.503 53.805 51.603 49.155 47.643 160 58.077 57.977 56.981 55.246 52.996 50.494 48.947 165 59.570 59.469 58.452 56.681 54.384 51.827 50.247 170 61.058 60.954 59.916 58.110 55.766 53.156 51.542 175 62.539 62.433 61.375 59.534 57.143 54.479 52.832 180 64.014 63.906 62.829 60.952 58.514 55.798 54.118 185 65.484 65.374 64.276 62.365 59.881 57.112 55.399 190 66.948 66.836 65.718 63.773 61.243 58.422 56.676 195 68.406 68.293 67.156 65.175 62.600 59.727 57.949 200 69.860 69.744 68.588 66.573 63.952 61.028 59.217 205 71.309 71.191 70.015 67.967 65.301 62.326 60.482 210 72.752 72.633 71.437 69.355 66.645 63.619 61.744 215 74.191 74.070 72.855 70.740 67.985 64.908 63.001 220 75.626 75.503 74.269 72.120 69.321 66.194 64.255 225 77.056 76.931 75.678 73.496 70.653 67.476 65.506 230 78.482 78.355 77.083 74.868 71.981 68.755 66.753 235 79.903 79.774 78.484 76.236 73.306 70.030 67.997 240 81.321 81.190 79.881 77.601 74.627 71.302 69.238 245 82.734 82.602 81.275 78.962 75.945 72.570 70.476 250 84.144 84.010 82.664 80.319 77.259 73.736 71.711 255 85.550 85.414 84.050 81.672 78.570 75.098 72.943 260 86.952 86.814 85.432 83.023 79.878 76.358 74.172 265 88.351 88.211 86.811 84.369 81.182 77.614 75.398 270 89.746 89.604 88.186 85.713 82.484 78.868 76.621 275 91.138 90.994 89.558 87.053 83.782 80.119 77.842 280 92.526 92.381 90.926 88.391 85.078 81.367 79.060 285 93.911 93.764 92.292 89.725 86.371 82.612 80.276 290 95.293 95.144 93.654 91.056 87.660 83.855 81.489 (continued) 329 Table 9.6 Dimensionless Influx, WeD, for Infinite Aquifer for Bottomwater Drive (continued) z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 295 96.672 96.521 95.014 92.385 88.948 85.095 82.700 300 98.048 97.895 96.370 93.710 90.232 86.333 83.908 305 99.420 99.266 97.724 95.033 91.514 87.568 85.114 310 100.79 100.64 99.07 96.35 92.79 88.80 86.32 315 102.16 102.00 100.42 97.67 94.07 90.03 87.52 320 103.52 103.36 101.77 98.99 95.34 91.26 88.72 325 104.88 104.72 103.11 100.30 96.62 92.49 89.92 330 106.24 106.08 104.45 101.61 97.89 93.71 91.11 335 107.60 107.43 105.79 102.91 99.15 94.93 92.30 340 108.95 108.79 107.12 104.22 100.42 96.15 93.49 345 110.30 110.13 108.45 105.52 101.68 97.37 94.68 350 111.65 111.48 109.78 106.82 102.94 98.58 95.87 355 113.00 112.82 111.11 108.12 104.20 99.80 97.06 360 114.34 114.17 112.43 109.41 105.45 101.01 98.24 365 115.68 115.51 113.76 110.71 106.71 102.22 99.42 370 117.02 116.84 115.08 112.00 107.96 103.42 100.60 375 118.36 118.18 116.40 113.29 109.21 104.63 101.78 380 119.69 119.51 117.71 114.57 110.46 105.83 102.95 385 121.02 120.84 119.02 115.86 111.70 107.04 104.13 390 122.35 122.17 120.34 117.14 112.95 108.24 105.30 395 123.68 123.49 121.65 118.42 114.19 109.43 106.47 400 125.00 124.82 122.94 119.70 115.43 110.63 107.64 405 126.33 126.14 124.26 120.97 116.67 111.82 108.80 410 127.65 127.46 125.56 122.25 117.90 113.02 109.97 415 128.97 128.78 126.86 123.52 119.14 114.21 111.13 420 130.28 130.09 128.16 124.79 120.37 115.40 112.30 425 131.60 131.40 129.46 126.06 121.60 116.59 113.46 430 132.91 132.72 130.75 127.33 122.83 117.77 114.62 435 134.22 134.03 132.05 128.59 124.06 118.96 115.77 440 135.53 135.33 133.34 129.86 125.29 120.14 116.93 445 136.84 136.64 134.63 131.12 126.51 121.32 118.08 450 138.15 137.94 135.92 132.38 127.73 122.50 119.24 455 139.45 139.25 137.20 133.64 128.96 123.68 120.39 460 140.75 140.55 138.49 134.90 130.18 124.86 121.54 330 z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 465 142.05 141.85 139.77 136.15 131.39 126.04 122.69 470 143.35 143.14 141.05 137.40 132.61 127.21 123.84 475 144.65 144.44 142.33 138.66 133.82 128.38 124.98 480 145.94 145.73 143.61 139.91 135.04 129.55 126.13 485 147.24 147.02 144.89 141.15 136.25 130.72 127.27 490 148.53 148.31 146.16 142.40 137.46 131.89 128.41 495 149.82 149.60 147.43 143.65 138.67 133.06 129.56 500 151.11 150.89 148.71 144.89 139.88 134.23 130.70 510 153.68 153.46 151.24 147.38 142.29 136.56 132.97 520 156.25 156.02 153.78 149.85 144.70 138.88 135.24 530 158.81 158.58 156.30 152.33 147.10 141.20 137.51 540 161.36 161.13 158.82 154.79 149.49 143.51 139.77 550 163.91 163.68 161.34 157.25 151.88 145.82 142.03 560 166.45 166.22 163.85 159.71 154.27 148.12 144.28 570 168.99 168.75 166.35 162.16 156.65 150.42 146.53 580 171.52 171.28 168.85 164.61 159.02 152.72 148.77 590 174.05 173.80 171.34 167.05 161.39 155.01 151.01 600 176.57 176.32 173.83 169.48 163.76 157.29 153.25 610 179.09 178.83 176.32 171.92 166.12 159.58 155.48 620 181.60 181.34 178.80 174.34 168.48 161.85 157.71 630 184.10 183.85 181.27 176.76 170.83 164.13 159.93 640 186.60 186.35 183.74 179.18 173.18 166.40 162.15 650 189.10 188.84 186.20 181.60 175.52 168.66 164.37 660 191.59 191.33 188.66 184.00 177.86 170.92 166.58 670 194.08 193.81 191.12 186.41 180.20 173.18 168.79 680 196.57 196.29 193.57 188.81 182.53 175.44 170.99 690 199.04 198.77 196.02 191.21 184.86 177.69 173.20 700 201.52 201.24 198.46 193.60 187.19 179.94 175.39 710 203.99 203.71 200.90 195.99 189.51 182.18 177.59 720 206.46 206.17 203.34 198.37 191.83 184.42 179.78 730 208.92 208.63 205.77 200.75 194.14 186.66 181.97 740 211.38 211.09 208.19 203.13 196.45 188.89 184.15 750 213.83 213.54 210.62 205.50 198.76 191.12 186.34 760 216.28 215.99 213.04 207.87 201.06 193.35 188.52 770 218.73 218.43 215.45 210.24 203.36 195.57 190.69 (continued) 331 Table 9.6 Dimensionless Influx, WeD, for Infinite Aquifer for Bottomwater Drive (continued) z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 780 221.17 220.87 217.86 212.60 205.66 197.80 192.87 790 223.61 223.31 220.27 214.96 207.95 200.01 195.04 800 226.05 225.74 222.68 217.32 210.24 202.23 197.20 810 228.48 228.17 225.08 219.67 212.53 204.44 199.37 820 230.91 230.60 227.48 222.02 214.81 206.65 201.53 830 233.33 233.02 229.87 224.36 217.09 208.86 203.69 840 235.76 235.44 232.26 226.71 219.37 211.06 205.85 850 238.18 237.86 234.65 229.05 221.64 213.26 208.00 860 240.59 240.27 237.04 231.38 223.92 215.46 210.15 870 243.00 242.68 239.42 233.72 226.19 217.65 212.30 880 245.41 245.08 241.80 236.05 228.45 219.85 214.44 890 247.82 247.49 244.17 238.37 230.72 222.04 216.59 900 250.22 249.89 246.55 240.70 232.98 224.22 218.73 910 252.62 252.28 248.92 243.02 235.23 226.41 220.87 920 255.01 254.68 251.28 245.34 237.49 228.59 223.00 930 257.41 257.07 253.65 247.66 239.74 230.77 225.14 940 259.80 259.46 256.01 249.97 241.99 232.95 227.27 950 262.19 261.84 258.36 252.28 244.24 235.12 229.39 960 264.57 264.22 260.72 254.59 246.48 237.29 231.52 970 266.95 266.60 263.07 256.89 248.72 239.46 233.65 980 269.33 268.98 265.42 259.19 250.96 241.63 235.77 990 271.71 271.35 267.77 261.49 253.20 243.80 237.89 1000 274.08 273.72 270.11 263.79 255.44 245.96 240.00 1010 276.35 275.99 272.35 265.99 257.58 248.04 242.04 1020 278.72 278.35 274.69 268.29 259.81 250.19 244.15 1030 281.08 280.72 277.03 270.57 262.04 252.35 246.26 1040 283.44 283.08 279.36 272.86 264.26 254.50 248.37 1050 285.81 285.43 281.69 275.15 266.49 256.66 250.48 1060 288.16 287.79 284.02 277.43 268.71 258.81 252.58 1070 290.52 290.14 286.35 279.71 270.92 260.95 254.69 1080 292.87 292.49 288.67 281.99 273.14 263.10 256.79 1090 295.22 294.84 290.99 284.26 275.35 265.24 258.89 1100 297.57 297.18 293.31 286.54 277.57 267.38 260.98 1110 299.91 299.53 295.63 288.81 279.78 269.52 263.08 332 z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 1120 302.26 301.87 297.94 291.07 281.98 271.66 265.17 1130 304.60 304.20 300.25 293.34 284.19 273.80 267.26 1140 306.93 306.54 302.56 295.61 286.39 275.93 269.35 1150 309.27 308.87 304.87 297.87 288.59 278.06 271.44 1160 311.60 311.20 307.18 300.13 290.79 280.19 273.52 1170 313.94 313.53 309.48 302.38 292.99 282.32 275.61 1180 316.26 315.86 311.78 304.64 295.19 284.44 277.69 1190 318.59 318.18 314.08 306.89 297.38 286.57 279.77 1200 320.92 320.51 316.38 309.15 299.57 288.69 281.85 1210 323.24 322.83 318.67 311.39 301.76 290.81 283.92 1220 325.56 325.14 320.96 313.64 303.95 292.93 286.00 1230 327.88 327.46 323.25 315.89 306.13 295.05 288.07 1240 330.19 329.77 325.54 318.13 308.32 297.16 290.14 1250 332.51 332.08 327.83 320.37 310.50 229.27 292.21 1260 334.82 334.39 330.11 322.61 312.68 301.38 294.28 1270 337.13 336.70 332.39 324.85 314.85 303.49 296.35 1280 339.44 339.01 334.67 327.08 317.03 305.60 298.41 1290 341.74 341.31 336.95 329.32 319.21 307.71 300.47 1300 344.05 343.61 339.23 331.55 321.38 309.81 302.54 1310 346.35 345.91 341.50 333.78 323.55 311.92 304.60 1320 348.65 348.21 343.77 336.01 325.72 314.02 306.65 1330 350.95 350.50 346.04 338.23 327.89 316.12 308.71 1340 353.24 352.80 348.31 340.46 330.05 318.22 310.77 1350 355.54 355.09 350.58 342.68 332.21 320.31 312.82 1360 357.83 357.38 352.84 344.90 334.38 322.41 314.87 1370 360.12 359.67 355.11 347.12 336.54 324.50 316.92 1380 362.41 361.95 357.37 349.34 338.70 326.59 318.97 1390 364.69 364.24 359.63 351.56 340.85 328.68 321.02 1400 366.98 366.52 361.88 353.77 343.01 330.77 323.06 1410 369.26 368.80 364.14 355.98 345.16 332.86 325.11 1420 371.54 371.08 366.40 358.19 347.32 334.94 327.15 1430 373.82 373.35 368.65 360.40 349.47 337.03 329.19 1440 376.10 375.63 370.90 362.61 351.62 339.11 331.23 1450 378.38 377.90 373.15 364.81 353.76 341.19 333.27 1460 380.65 380.17 375.39 367.02 355.91 343.27 335.31 (continued) 333 Table 9.6 Dimensionless Influx, WeD, for Infinite Aquifer for Bottomwater Drive (continued) z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 1470 382.92 382.44 377.64 369.22 358.06 345.35 337.35 1480 385.19 384.71 379.88 371.42 360.20 347.43 339.38 1490 387.46 386.98 382.13 373.62 362.34 349.50 341.42 1500 389.73 389.25 384.37 375.82 364.48 351.58 343.45 1525 395.39 394.90 389.96 381.31 369.82 356.76 348.52 1550 401.04 400.55 395.55 386.78 375.16 361.93 353.59 1575 406.68 406.18 401.12 392.25 380.49 367.09 358.65 1600 412.32 411.81 406.69 397.71 385.80 372.24 363.70 1625 417.94 417.42 412.24 403.16 391.11 377.39 368.74 1650 423.55 423.03 417.79 408.60 396.41 382.53 373.77 1675 429.15 428.63 423.33 414.04 401.70 387.66 378.80 1700 434.75 434.22 428.85 419.46 406.99 392.78 383.82 1725 440.33 439.79 434.37 424.87 412.26 397.89 388.83 1750 445.91 445.37 439.89 430.28 417.53 403.00 393.84 1775 451.48 450.93 445.39 435.68 422.79 408.10 398.84 1800 457.04 456.48 450.88 441.07 428.04 413.20 403.83 1825 462.59 462.03 456.37 446.46 433.29 418.28 408.82 1850 468.13 467.56 461.85 451.83 438.53 423.36 413.80 1875 473.67 473.09 467.32 457.20 443.76 428.43 418.77 1900 479.19 478.61 472.78 462.56 448.98 433.50 423.73 1925 484.71 484.13 478.24 467.92 454.20 438.56 428.69 1950 490.22 489.63 483.69 473.26 459.41 443.61 433.64 1975 495.73 495.13 489.13 478.60 464.61 448.66 438.59 2000 501.22 500.62 494.56 483.93 469.81 453.70 443.53 2025 506.71 506.11 499.99 489.26 475.00 458.73 448.47 2050 512.20 511.58 505.41 494.58 480.18 463.76 453.40 2075 517.67 517.05 510.82 499.89 485.36 468.78 458.32 2100 523.14 522.52 516.22 505.19 490.53 473.80 463.24 2125 528.60 527.97 521.62 510.49 495.69 478.81 468.15 2150 534.05 533.42 527.02 515.78 500.85 483.81 473.06 2175 539.50 538.86 532.40 521.07 506.01 488.81 477.96 2200 544.94 544.30 537.78 526.35 511.15 493.81 482.85 2225 550.38 549.73 543.15 531.62 516.29 498.79 487.74 2250 555.81 555.15 548.52 536.89 521.43 503.78 492.63 334 z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 2275 561.23 560.56 553.88 542.15 526.56 508.75 497.51 2300 566.64 565.97 559.23 547.41 531.68 513.72 502.38 2325 572.05 571.38 564.58 552.66 536.80 518.69 507.25 2350 577.46 576.78 569.92 557.90 541.91 523.65 512.12 2375 582.85 582.17 575.26 563.14 547.02 528.61 516.98 2400 588.24 587.55 580.59 568.37 552.12 533.56 521.83 2425 593.63 592.93 585.91 573.60 557.22 538.50 526.68 2450 599.01 598.31 591.23 578.82 562.31 543.45 531.53 2475 604.38 603.68 596.55 584.04 567.39 548.38 536.37 2500 609.75 609.04 601.85 589.25 572.47 553.31 541.20 2550 620.47 619.75 612.45 599.65 582.62 563.16 550.86 2600 631.17 630.43 623.03 610.04 592.75 572.99 560.50 2650 641.84 641.10 633.59 620.40 602.86 582.80 570.13 2700 652.50 651.74 644.12 630.75 612.95 592.60 579.73 2750 663.13 662.37 654.64 641.07 623.02 602.37 589.32 2800 673.75 672.97 665.14 651.38 633.07 612.13 598.90 2850 684.34 683.56 675.61 661.67 643.11 621.88 608.45 2900 694.92 694.12 686.07 671.94 653.12 631.60 617.99 2950 705.48 704.67 696.51 682.19 663.13 641.32 627.52 3000 716.02 715.20 706.94 692.43 673.11 651.01 637.03 3050 726.54 725.71 717.34 702.65 683.08 660.69 646.53 3100 737.04 736.20 727.73 712.85 693.03 670.36 656.01 3150 747.53 746.68 738.10 723.04 702.97 680.01 665.48 3200 758.00 757.14 748.45 733.21 712.89 689.64 674.93 3250 768.45 767.58 758.79 743.36 722.80 699.27 684.37 3300 778.89 778.01 769.11 753.50 732.69 708.87 693.80 3350 789.31 788.42 779.42 763.62 742.57 718.47 703.21 3400 799.71 798.81 789.71 773.73 752.43 728.05 712.62 3450 810.10 809.19 799.99 783.82 762.28 737.62 722.00 3500 820.48 819.55 810.25 793.90 772.12 747.17 731.38 3550 830.83 829.90 820.49 803.97 781.94 756.72 740.74 3600 841.18 840.24 830.73 814.02 791.75 766.24 750.09 3650 851.51 850.56 840.94 824.06 801.55 775.76 759.43 3700 861.83 860.86 851.15 834.08 811.33 785.27 768.76 3750 872.13 871.15 861.34 844.09 821.10 794.76 778.08 (continued) 335 Table 9.6 Dimensionless Influx, WeD, for Infinite Aquifer for Bottomwater Drive (continued) z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 3800 882.41 881.43 871.51 854.09 830.86 804.24 787.38 3850 892.69 891.70 881.68 864.08 840.61 813.71 796.68 3900 902.95 901.95 891.83 874.05 850.34 823.17 805.96 3950 913.20 912.19 901.96 884.01 860.06 832.62 815.23 4000 923.43 922.41 912.09 893.96 869.77 842.06 824.49 4050 933.65 932.62 922.20 903.89 879.47 851.48 833.74 4100 943.86 942.82 932.30 913.82 889.16 860.90 842.99 4150 954.06 953.01 942.39 923.73 898.84 870.30 852.22 4200 964.25 963.19 952.47 933.63 908.50 879.69 861.44 4250 974.42 973.35 962.53 943.52 918.16 889.08 870.65 4300 984.58 983.50 972.58 953.40 927.80 898.45 879.85 4350 994.73 993.64 982.62 963.27 937.42 907.81 889.04 4400 1004.9 1003.8 992.7 973.1 947.1 917.2 898.2 4450 1015.0 1013.9 1002.7 983.0 956.7 926.5 907.4 4500 1025.1 1024.0 1012.7 992.8 966.3 935.9 916.6 4550 1035.2 1034.1 1022.7 1002.6 975.9 945.2 925.7 4600 1045.3 1044.2 1032.7 1012.4 985.5 954.5 934.9 4650 1055.4 1054.2 1042.6 1022.2 995.0 963.8 944.0 4700 1065.5 1064.3 1052.6 1032.0 1004.6 973.1 953.1 4750 1075.5 1074.4 1062.6 1041.8 1014.1 982.4 962.2 4800 1085.6 1084.4 1072.5 1051.6 1023.7 991.7 971.4 4850 1095.6 1094.4 1082.4 1061.4 1033.2 1000.9 980.5 4900 1105.6 1104.5 1092.4 1071.1 1042.8 1010.2 989.5 4950 1115.7 1114.5 1102.3 1080.9 1052.3 1019.4 998.6 5000 1125.7 1124.5 1112.2 1090.6 1061.8 1028.7 1007.7 5100 1145.7 1144.4 1132.0 1110.0 1080.8 1047.2 1025.8 5200 1165.6 1164.4 1151.7 1129.4 1099.7 1065.6 1043.9 5300 1185.5 1184.3 1171.4 1148.8 1118.6 1084.0 1062.0 5400 1205.4 1204.1 1191.1 1168.2 1137.5 1102.4 1080.0 5500 1225.3 1224.0 1210.7 1187.5 1156.4 1120.7 1098.0 5600 1245.1 1243.7 1230.3 1206.7 1175.2 1139.0 1116.0 5700 1264.9 1263.5 1249.9 1226.0 1194.0 1157.3 1134.0 5800 1284.6 1283.2 1269.4 1245.2 1212.8 1175.5 1151.9 5900 1304.3 1302.9 1288.9 1264.4 1231.5 1193.8 1169.8 336 z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 6000 1324.0 1322.6 1308.4 1283.5 1250.2 1211.9 1187.7 6100 1343.6 1342.2 1327.9 1302.6 1268.9 1230.1 1205.5 6200 1363.2 1361.8 1347.3 1321.7 1287.5 1248.3 1223.3 6300 1382.8 1381.4 1366.7 1340.8 1306.2 1266.4 1241.1 6400 1402.4 1400.9 1386.0 1359.8 1324.7 1284.5 1258.9 6500 1421.9 1420.4 1405.3 1378.8 1343.3 1302.5 1276.6 6600 1441.4 1439.9 1424.6 1397.8 1361.9 1320.6 1294.3 6700 1460.9 1459.4 1443.9 1416.7 1380.4 1338.6 1312.0 6800 1480.3 1478.8 1463.1 1435.6 1398.9 1356.6 1329.7 6900 1499.7 1498.2 1482.4 1454.5 1417.3 1374.5 1347.4 7000 1519.1 1517.5 1501.5 1473.4 1435.8 1392.5 1365.0 7100 1538.5 1536.9 1520.7 1492.3 1454.2 1410.4 1382.6 7200 1557.8 1556.2 1539.8 1511.1 1472.6 1428.3 1400.2 7300 1577.1 1575.5 1559.0 1529.9 1491.2 1446.2 1417.8 7400 1596.4 1594.8 1578.1 1548.6 1509.3 1464.1 1435.3 7500 1615.7 1614.0 1597.1 1567.4 1527.6 1481.9 1452.8 7600 1634.9 1633.2 1616.2 1586.1 1545.9 1499.7 1470.3 7700 1654.1 1652.4 1635.2 1604.8 1564.2 1517.5 1487.8 7800 1673.3 1671.6 1654.2 1623.5 1582.5 1535.3 1505.3 7900 1692.5 1690.7 1673.1 1642.2 1600.7 1553.0 1522.7 8000 1711.6 1709.9 1692.1 1660.8 1619.0 1570.8 1540.1 8100 1730.8 1729.0 1711.0 1679.4 1637.2 1588.5 1557.6 8200 1749.9 1748.1 1729.9 1698.0 1655.3 1606.2 1574.9 8300 1768.9 1767.1 1748.8 1716.6 1673.5 1623.9 1592.3 8400 1788.0 1786.2 1767.7 1735.2 1691.6 1641.5 1609.7 8500 1807.0 1805.2 1786.5 1753.7 1709.8 1659.2 1627.0 8600 1826.0 1824.2 1805.4 1722.2 1727.9 1676.8 1644.3 8700 1845.0 1843.2 1824.2 1790.7 1746.0 1694.4 1661.6 8800 1864.0 1862.1 1842.9 1809.2 1764.0 1712.0 1678.9 8900 1833.0 1881.1 1861.7 1827.7 1782.1 1729.6 1696.2 9900 1901.9 1900.0 1880.5 1846.0 1800.1 1747.1 1713.4 9100 1920.8 1918.9 1889.2 1864.5 1818.1 1764.7 1730.7 9200 1939.7 1937.4 1917.9 1882.9 1836.1 1782.2 1747.9 9300 1958.6 1956.6 1936.6 1901.3 1854.1 1799.7 1765.1 9400 1977.4 1975.4 1955.2 1919.7 1872.0 1817.2 1782.3 (continued) 337 Table 9.6 Dimensionless Influx, WeD, for Infinite Aquifer for Bottomwater Drive (continued) z D′ 0.05 tD 0.1 0.3 0.5 0.7 0.9 1.0 9500 1996.3 1994.3 1973.9 1938.0 1890.0 1834.7 1799.4 9600 2015.1 2013.1 1992.5 1956.4 1907.9 1852.1 1816.6 9700 2033.9 2031.9 2011.1 1974.7 1925.8 1869.6 1833.7 9800 2052.7 2050.6 2029.7 1993.0 1943.7 1887.0 1850.9 9900 1.00×10 2071.5 4 2069.4 2.090×10 3 2048.3 2.088×10 3 2011.3 2.067×10 3 1961.6 2.029×10 3 1904.4 1.979×10 3 1868.0 3 1.922×10 1.855×103 1.25×104 2.553×103 2.551×103 2.526×103 2.481×103 2.421×103 2.352×103 2.308×103 1.50×10 3.009×10 3.006×10 2.977×10 2.925×10 2.855×10 2.775×10 3 2.724×103 4 3 3 3 3 3 1.75×104 3.457×103 3.454×103 3.421×103 3.362×103 3.284×103 3.193×103 3.135×103 2.00×10 3.900×10 3.897×10 3.860×10 3.794×10 3.707×10 3.605×10 3 3.541×103 4 3 3 3 3 3 2.50×104 4.773×103 4.768×103 4.724×103 4.646×103 4.541×103 4.419×103 4.341×103 3.00×10 5.630×10 5.625×10 5.574×10 5.483×10 5.361×10 5.219×10 3 5.129×103 4 3 3 3 3 3 3.50×104 6.476×103 6.470×103 6.412×103 6.309×103 6.170×103 6.009×103 5.906×103 4.00×10 7.312×10 7.305×10 7.240×10 7.125×10 6.970×10 6.790×10 3 6.675×103 4.50×104 8.139×103 8.132×103 8.060×103 7.933×103 7.762×103 7.564×103 7.437×103 5.00×104 8.959×103 8.951×103 8.872×103 8.734×103 8.548×103 8.331×103 8.193×103 6.00×10 1.057×10 1.057×10 1.047×10 1.031×10 1.010×10 9.846×10 3 9.684×103 4 4 3 4 3 4 3 4 3 4 3 4 7.00×104 1.217×104 1.217×104 1.206×104 1.188×104 1.163×104 1.134×104 1.116×104 8.00×10 1.375×10 1.375×10 1.363×10 1.342×10 1.315×10 1.283×10 4 1.262×104 4 4 4 4 4 4 9.00×104 1.532×104 1.531×104 1.518×104 1.496×104 1.465×104 1.430×104 1.407×104 1.00×10 1.687×10 1.686×10 1.672×10 1.647×10 1.614×10 1.576×10 4 1.551×104 1.25×105 2.071×104 2.069×104 2.052×104 2.023×104 1.982×104 1.936×104 1.906×104 1.50×105 2.448×104 2.446×104 2.427×104 2.392×104 2.345×104 2.291×104 2.256×104 2.00×10 3.190×10 3.188×10 3.163×10 3.119×10 3.059×10 2.989×10 4 2.945×104 5 5 4 4 4 4 4 4 4 4 4 4 2.50×105 3.918×104 3.916×104 3.885×104 3.832×104 3.760×104 3.676×104 3.622×104 3.00×10 4.636×10 4.633×10 4.598×10 4.536×10 4.452×10 4.353×10 4 4.290×104 5 4 4 4 4 4 4.00×105 6.048×104 6.004×104 5.999×104 5.920×104 5.812×104 5.687×104 5.606×104 5.00×10 7.436×10 7.431×10 7.376×10 7.280×10 7.150×10 6.998×10 4 6.900×104 5 4 4 4 4 4 6.00×105 8.805×104 8.798×104 8.735×104 8.623×104 8.471×104 8.293×104 8.178×104 7.00×10 1.016×10 1.015×10 1.008×10 9.951×10 9.777×10 9.573×10 4 9.442×104 8.00×105 1.150×105 1.149×105 1.141×105 1.127×105 1.107×105 1.084×105 1.070×105 9.00×105 1.283×105 1.282×105 1.273×105 1.257×105 1.235×105 1.210×105 1.194×105 1.00×10 1.415×10 1.412×10 1.404×10 1.387×10 1.363×10 1.335×10 5 1.317×105 1.50×106 2.059×105 2.060×105 2.041×105 2.016×105 1.982×105 1.943×105 1.918×105 5 6 5 5 5 5 5 5 4 5 338 4 5 z D′ 0.05 tD 2.00×10 0.1 0.3 0.5 0.7 0.9 1.0 2.695×10 2.695×10 2.676×10 2.644×10 2.601×10 2.551×10 2.518×105 2.50×106 3.320×105 3.319×105 3.296×105 3.254×105 3.202×105 3.141×105 3.101×105 3.00×106 3.937×105 3.936×105 3.909×105 3.864×105 3.803×105 3.731×105 3.684×105 4.00×10 5.154×10 5.152×10 5.118×10 5.060×10 4.981×10 4.888×10 5 4.828×105 6 6 5 5 5 5 5 5 5 5 5 5 5 5.00×106 6.352×105 6.349×105 6.308×105 6.238×105 6.142×105 6.029×105 5.956×105 6.00×10 7.536×10 7.533×10 7.485×10 7.402×10 7.290×10 7.157×10 5 7.072×105 6 5 5 5 5 5 7.00×106 8.709×105 8.705×105 8.650×105 8.556×105 8.427×105 8.275×105 8.177×105 8.00×10 9.972×10 9.867×10 9.806×10 9.699×10 9.555×10 9.384×10 5 9.273×105 6 5 5 5 5 5 9.00×106 1.103×106 1.102×106 1.095×106 1.084×106 1.067×106 1.049×106 1.036×106 1.00×10 1.217×10 1.217×10 1.209×10 1.196×10 1.179×10 1.158×10 6 1.144×106 1.50×107 1.782×106 1.781×106 1.771×106 1.752×106 1.727×106 1.697×106 1.678×106 2.00×107 2.337×106 2.336×106 2.322×106 2.298×106 2.266×106 2.227×106 2.202×106 2.50×10 2.884×10 2.882×10 2.866×10 2.837×10 2.797×10 2.750×10 6 2.720×106 7 7 6 6 6 6 6 6 6 6 6 6 3.00×107 3.425×106 3.423×106 3.404×106 3.369×106 3.323×106 3.268×106 3.232×106 4.00×10 4.493×10 4.491×10 4.466×10 4.422×10 4.361×10 4.290×10 6 4.244×106 7 6 6 6 6 6 5.00×107 5.547×106 5.544×106 5.514×106 5.460×106 5.386×106 5.299×106 5.243×106 6.00×10 6.590×10 6.587×10 6.551×10 6.488×10 6.401×10 6.299×10 6 6.232×106 7.00×107 7.624×106 7.620×106 7.579×106 7.507×106 7.407×106 7.290×106 7.213×106 8.00×107 8.651×106 8.647×106 8.600×106 8.519×106 8.407×106 8.274×106 8.188×106 9.00×10 9.671×10 9.666×10 9.615×10 9.524×10 9.400×10 9.252×10 6 9.156×106 7 7 6 6 6 6 6 6 6 6 6 6 1.00×108 1.069×107 1.067×107 1.062×107 1.052×107 1.039×107 1.023×107 1.012×107 1.50×10 1.567×10 1.567×10 1.555×10 1.541×10 1.522×10 1.499×10 7 1.483×107 8 7 7 7 7 7 2.00×108 2.059×107 2.059×107 2.048×107 2.029×107 2.004×107 1.974×107 1.954×107 2.50×10 2.546×10 2.545×10 2.531×10 2.507×10 2.476×10 2.439×10 7 2.415×107 8 7 7 7 7 7 3.00×108 3.027×107 3.026×107 3.010×107 2.984×107 2.947×107 2.904×107 2.875×107 4.00×10 3.979×10 3.978×10 3.958×10 3.923×10 3.875×10 3.819×10 7 3.782×107 5.00×108 4.920×107 4.918×107 4.894×107 4.851×107 4.793×107 4.724×107 4.679×107 6.00×108 5.852×107 5.850×107 5.821×107 5.771×107 5.702×107 5.621×107 5.568×107 7.00×10 6.777×10 6.774×10 6.741×10 6.684×10 6.605×10 6.511×10 7 6.450×107 8 8 7 7 7 7 7 7 7 7 7 7 8.00×108 7.700×107 7.693×107 7.655×107 7.590×107 7.501×107 7.396×107 7.327×107 9.00×10 8.609×10 8.606×10 8.564×10 8.492×10 8.393×10 8.275×10 7 8.199×107 8 7 7 7 7 7 1.00×109 9.518×107 9.515×107 9.469×107 9.390×107 9.281×107 9.151×107 9.066×107 1.50×10 1.401×10 1.400×10 1.394×10 1.382×10 1.367×10 1.348×10 8 1.336×108 2.00×109 1.843×108 1.843×108 1.834×108 1.819×108 1.799×108 1.774×108 1.758×108 2.50×109 2.281×108 2.280×108 2.269×108 2.251×108 2.226×108 2.196×108 2.177×108 9 8 8 8 8 8 (continued) 339 Table 9.6 Dimensionless Influx, WeD, for Infinite Aquifer for Bottomwater Drive (continued) z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 3.00×109 2.714×108 2.713×108 2.701×108 2.680×108 2.650×108 2.615×108 2.592×108 4.00×109 3.573×108 3.572×108 3.556×108 3.528×108 3.489×108 3.443×108 3.413×108 5.00×109 4.422×108 4.421×108 4.401×108 4.367×108 4.320×108 4.263×108 4.227×108 6.00×10 5.265×10 5.262×10 5.240×10 5.199×10 5.143×10 5.077×10 8 5.033×108 9 8 8 8 8 8 7.00×109 6.101×108 6.098×108 6.072×108 6.025×108 5.961×108 5.885×108 5.835×108 8.00×10 6.932×10 6.930×10 6.900×10 6.847×10 6.775×10 6.688×10 8 6.632×108 9.00×109 7.760×108 7.756×108 7.723×108 7.664×108 7.584×108 7.487×108 7.424×108 1.00×1010 8.583×108 8.574×108 8.543×108 8.478×108 8.389×108 8.283×108 8.214×108 1.50×10 1.263×10 1.264×10 1.257×10 1.247×10 1.235×10 1.219×10 9 1.209×109 9 10 8 9 8 9 8 9 8 9 8 9 2.00×1010 1.666×109 1.666×109 1.659×109 1.646×109 1.630×109 1.610×109 1.596×109 2.50×10 2.065×10 2.063×10 2.055×10 2.038×10 2.018×10 1.993×10 9 1.977×109 10 9 9 9 9 9 3.00×1010 2.458×109 2.458×109 2.447×109 2.430×109 2.405×109 2.376×109 2.357×109 4.00×10 3.240×10 3.239×10 3.226×10 3.203×10 3.171×10 3.133×10 9 3,108×109 5.00×1010 4.014×109 4.013×109 3.997×109 3.968×109 3.929×109 3.883×109 3.852×109 6.00×1010 4.782×109 4.781×109 4.762×109 4.728×109 4.682×109 4.627×109 4.591×109 7.00×10 5.546×10 5.544×10 5.522×10 5.483×10 5.430×10 5.366×10 9 5.325×109 10 10 9 9 9 9 9 9 9 9 9 9 8.00×1010 6.305×109 6.303×109 6.278×109 6.234×109 6.174×109 6.102×109 6.055×109 9.00×10 7.060×10 7.058×10 7.030×10 6.982×10 6.914×10 6.834×10 9 6.782×109 1.00×1011 7.813×109 7.810×109 7.780×109 7.726×109 7.652×109 7.564×109 7.506×109 1.50×10 1.154×10 1.153×10 1.149×10 1.141×10 1.130×10 1.118×10 10 1.109×1010 10 11 9 10 9 10 9 10 9 10 9 10 2.00×1011 1.522×1010 1.521×1010 1.515×1010 1.505×1010 1.491×1010 1.474×1010 1.463×1010 2.50×10 1.886×10 1.885×10 1.878×10 1.866×10 1.849×10 1.828×10 10 1.814×1010 3.00×1011 2.248×1010 2.247×1010 2.239×1010 2.224×1010 2.204×1010 2.179×1010 2.163×1010 4.00×1011 2.965×1010 2.964×1010 2.953×1010 2.934×1010 2.907×1010 2.876×1010 2.855×1010 5.00×10 3.677×10 3.675×10 3.662×10 3.638×10 3.605×10 3.566×10 10 3.540×1010 11 11 10 10 10 10 10 10 10 10 10 10 6.00×1011 4.383×1010 4.381×1010 4.365×1010 4.337×1010 4.298×1010 4.252×1010 4.221×1010 7.00×10 5.085×10 5.082×10 5.064×10 5.032×10 4.987×10 4.933×10 10 4.898×1010 11 10 10 10 10 10 8.00×1011 5.783×1010 5.781×1010 5.760×1010 5.723×1010 5.673×1010 5.612×1010 5.572×1010 9.00×10 6.478×10 6.476×10 6.453×10 6.412×10 6.355×10 6.288×10 10 6.243×1010 1.00×1012 7.171×1010 7.168×1010 7.143×1010 7.098×1010 7.035×1010 6.961×1010 6.912×1010 1.50×1012 1.060×1011 1.060×1011 1.056×1011 1.050×1011 1.041×1011 1.030×1011 1.022×1011 2.00×10 1.400×10 1.399×10 1.394×10 1.386×10 1.374×10 1.359×10 1.350×1011 11 12 10 11 10 11 10 11 10 11 340 10 11 11 Table 9.7 Dimensionless Influx, WeD, for rD′ = 4 for Bottomwater Drive z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 2 2.398 2.389 2.284 2.031 1.824 1.620 1.507 3 3.006 2.993 2.874 2.629 2.390 2.149 2.012 4 3.552 3.528 3.404 3.158 2.893 2.620 2.466 5 4.053 4.017 3.893 3.627 3.341 3.045 2.876 6 4.490 4.452 4.332 4.047 3.744 3.430 3.249 7 4.867 4.829 4.715 4.420 4.107 3.778 3.587 8 5.191 5.157 5.043 4.757 4.437 4.096 3.898 9 5.464 5.434 5.322 5.060 4.735 4.385 4.184 10 5.767 5.739 5.598 5.319 5.000 4.647 4.443 11 5.964 5.935 5.829 5.561 5.240 4.884 4.681 12 6.188 6.158 6.044 5.780 5.463 5.107 4.903 13 6.380 6.350 6.240 5.983 5.670 5.316 5.113 14 6.559 6.529 6.421 6.171 5.863 5.511 5.309 15 6.725 6.694 6.589 6.345 6.044 5.695 5.495 16 6.876 6.844 6.743 6.506 6.213 5.867 5.671 17 7.014 6.983 6.885 6.656 6.371 6.030 5.838 18 7.140 7.113 7.019 6.792 6.523 6.187 5.999 19 7.261 7.240 7.140 6.913 6.663 6.334 6.153 20 7.376 7.344 7.261 7.028 6.785 6.479 6.302 22 7.518 7.507 7.451 7.227 6.982 6.691 6.524 24 7.618 7.607 7.518 7.361 7.149 6.870 6.714 26 7.697 7.685 7.607 7.473 7.283 7.026 6.881 28 7.752 7.752 7.674 7.563 7.395 7.160 7.026 30 7.808 7.797 7.741 7.641 7.484 7.283 7.160 34 7.864 7.864 7.819 7.741 7.618 7.451 7.350 38 7.909 7.909 7.875 7.808 7.719 7.585 7.496 42 7.931 7.931 7.909 7.864 7.797 7.685 7.618 46 7.942 7.942 7.920 7.898 7.842 7.752 7.697 50 7.954 7.954 7.942 7.920 7.875 7.808 7.764 60 7.968 7.968 7.965 7.954 7.931 7.898 7.864 70 7.976 7.976 7.976 7.968 7.965 7.942 7.920 80 7.982 7.982 7.987 7.976 7.976 7.965 7.954 90 7.987 7.987 7.987 7.984 7.983 7.976 7.965 100 7.987 7.987 7.987 7.987 7.987 7.983 7.976 120 7.987 7.987 7.987 7.987 7.987 7.987 7.987 341 Table 9.8 Dimensionless Influx, WeD, for rD′ = 6 for Bottomwater Drive z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 6 4.780 4.762 4.597 4.285 3.953 3.611 3.414 7 5.309 5.289 5.114 4.779 4.422 4.053 3.837 8 5.799 5.778 5.595 5.256 4.875 4.478 4.247 9 6.252 6.229 6.041 5.712 5.310 4.888 4.642 10 6.750 6.729 6.498 6.135 5.719 5.278 5.019 11 7.137 7.116 6.916 6.548 6.110 5.648 5.378 12 7.569 7.545 7.325 6.945 6.491 6.009 5.728 13 7.967 7.916 7.719 7.329 6.858 6.359 6.067 14 8.357 8.334 8.099 7.699 7.214 6.697 6.395 15 8.734 8.709 8.467 8.057 7.557 7.024 6.713 16 9.093 9.067 8.819 8.398 7.884 7.336 7.017 17 9.442 9.416 9.160 8.730 8.204 7.641 7.315 18 9.775 9.749 9.485 9.047 8.510 7.934 7.601 19 10.09 10.06 9.794 9.443 8.802 8.214 7.874 20 10.40 10.37 10.10 9.646 9.087 8.487 8.142 22 10.99 10.96 10.67 10.21 9.631 9.009 8.653 24 11.53 11.50 11.20 10.73 10.13 9.493 9.130 26 12.06 12.03 11.72 11.23 10.62 9.964 9.594 28 12.52 12.49 12.17 11.68 11.06 10.39 10.01 30 12.95 12.92 12.59 12.09 11.46 10.78 10.40 35 13.96 13.93 13.57 13.06 12.41 11.70 11.32 40 14.69 14.66 14.33 13.84 13.23 12.53 12.15 45 15.27 15.24 14.94 14.48 13.90 13.23 12.87 50 15.74 15.71 15.44 15.01 14.47 13.84 13.49 60 16.40 16.38 16.15 15.81 15.34 14.78 14.47 70 16.87 16.85 16.67 16.38 15.99 15.50 15.24 80 17.20 17.18 17.04 16.80 16.48 16.06 15.83 90 17.43 17.42 17.30 17.10 16.85 16.50 16.29 100 17.58 17.58 17.49 17.34 17.12 16.83 16.66 110 17.71 17.69 17.63 17.50 17.34 17.09 16.93 120 17.78 17.78 17.73 17.63 17.49 17.29 17.17 130 17.84 17.84 17.79 17.73 17.62 17.45 17.34 140 17.88 17.88 17.85 17.79 17.71 17.57 17.48 150 17.92 17.91 17.88 17.84 17.77 17.66 17.58 175 17.95 17.95 17.94 17.92 17.87 17.81 17.76 342 z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 200 17.97 17.97 17.96 17.95 17.93 17.88 17.86 225 17.97 17.97 17.97 17.96 17.95 17.93 17.91 250 17.98 17.98 17.98 17.97 17.96 17.95 17.95 300 17.98 17.98 17.98 17.98 17.98 17.97 17.97 350 17.98 17.98 17.98 17.98 17.98 17.98 17.98 400 17.98 17.98 17.98 17.98 17.98 17.98 17.98 450 17.98 17.98 17.98 17.98 17.98 17.98 17.98 500 17.98 17.98 17.98 17.98 17.98 17.98 17.98 Table 9.9 Dimensionless Influx, WeD, for rD′ = 9 for Bottomwater Drive z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 9 6.301 6.278 6.088 5.756 5.350 4.924 4.675 10 6.828 6.807 6.574 6.205 5.783 5.336 5.072 11 7.250 7.229 7.026 6.650 6.204 5.732 5.456 12 7.725 7.700 7.477 7.086 6.621 6.126 5.836 13 8.173 8.149 7.919 7.515 7.029 6.514 6.210 14 8.619 8.594 8.355 7.937 7.432 6.895 6.578 15 9.058 9.032 8.783 8.351 7.828 7.270 6.940 16 9.485 9.458 9.202 8.755 8.213 7.634 7.293 17 9.907 9.879 9.613 9.153 8.594 7.997 7.642 18 10.32 10.29 10.01 9.537 8.961 8.343 7.979 19 10.72 10.69 10.41 9.920 9.328 8.691 8.315 20 11.12 11.08 10.80 10.30 9.687 9.031 8.645 22 11.89 11.86 11.55 11.02 10.38 9.686 9.280 24 12.63 12.60 12.27 11.72 11.05 10.32 9.896 26 13.36 13.32 12.97 12.40 11.70 10.94 10.49 28 14.06 14.02 13.65 13.06 12.33 11.53 11.07 30 14.73 14.69 14.30 13.68 12.93 12.10 11.62 34 16.01 15.97 15.54 14.88 14.07 13.18 12.67 38 17.21 17.17 16.70 15.99 15.13 14.18 13.65 40 17.80 17.75 17.26 16.52 15.64 14.66 14.12 45 19.15 19.10 18.56 17.76 16.83 15.77 15.21 50 20.42 20.36 19.76 18.91 17.93 16.80 16.24 343 (continued) Table 9.9 Dimensionless Influx, WeD, for rD′ = 9 for Bottomwater Drive (continued) z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 55 21.46 21.39 20.80 19.96 18.97 17.83 17.24 60 22.40 22.34 21.75 20.91 19.93 18.78 18.19 70 23.97 23.92 23.36 22.55 21.58 20.44 19.86 80 25.29 25.23 24.71 23.94 23.01 21.91 21.32 90 26.39 26.33 25.85 25.12 24.24 23.18 22.61 100 27.30 27.25 26.81 26.13 25.29 24.29 23.74 120 28.61 28.57 28.19 27.63 26.90 26.01 25.51 140 29.55 29.51 29.21 28.74 28.12 27.33 26.90 160 30.23 30.21 29.96 29.57 29.04 28.37 27.99 180 30.73 30.71 30.51 30.18 29.75 29.18 28.84 200 31.07 31.04 30.90 30.63 30.26 29.79 29.51 240 31.50 31.49 31.39 31.22 30.98 30.65 30.45 280 31.72 31.71 31.66 31.56 31.39 31.17 31.03 320 31.85 31.84 31.80 31.74 31.64 31.49 31.39 360 31.90 31.90 31.88 31.85 31.78 31.68 31.61 400 31.94 31.94 31.93 31.90 31.86 31.79 31.75 450 31.96 31.96 31.95 31.94 31.91 31.88 31.85 500 31.97 31.97 31.96 31.96 31.95 31.93 31.90 550 31.97 31.97 31.97 31.96 31.96 31.95 31.94 600 31.97 31.97 31.97 31.97 31.97 31.96 31.95 700 31.97 31.97 31.97 31.97 31.97 31.97 31.97 800 31.97 31.97 31.97 31.97 31.97 31.97 31.97 0.9 1.0 Table 9.10 Dimensionless Influx, WeD, for rD′ = 10 for Bottomwater Drive z D′ tD 0.05 0.1 0.3 0.5 0.7 22 12.07 12.04 11.74 11.21 10.56 9.865 9.449 24 12.86 12.83 12.52 11.97 11.29 10.55 10.12 26 13.65 13.62 13.29 12.72 12.01 11.24 10.78 28 14.42 14.39 14.04 13.44 12.70 11.90 11.42 30 15.17 15.13 14.77 14.15 13.38 12.55 12.05 344 z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 32 15.91 15.87 15.49 14.85 14.05 13.18 12.67 34 16.63 16.59 16.20 15.54 14.71 13.81 13.28 36 17.33 17.29 16.89 16.21 15.35 14.42 13.87 38 18.03 17.99 17.57 16.86 15.98 15.02 14.45 40 18.72 18.68 18.24 17.51 16.60 15.61 15.02 42 19.38 19.33 18.89 18.14 17.21 16.19 15.58 44 20.03 19.99 19.53 18.76 17.80 16.75 16.14 46 20.67 20.62 20.15 19.36 18.38 17.30 16.67 48 21.30 21.25 20.76 19.95 18.95 17.84 17.20 50 21.92 21.87 21.36 20.53 19.51 18.38 17.72 52 22.52 22.47 21.95 21.10 20.05 18.89 18.22 54 23.11 23.06 22.53 21.66 20.59 19.40 18.72 56 23.70 23.64 23.09 22.20 21.11 19.89 19.21 58 24.26 24.21 23.65 22.74 21.63 20.39 19.68 60 24.82 24.77 24.19 23.26 22.13 20.87 20.15 65 26.18 26.12 25.50 24.53 23.34 22.02 21.28 70 27.47 27.41 26.75 25.73 24.50 23.12 22.36 75 28.71 28.55 27.94 26.88 25.60 24.17 23.39 80 29.89 29.82 29.08 27.97 26.65 25.16 24.36 85 31.02 30.95 30.17 29.01 27.65 26.10 25.31 90 32.10 32.03 31.20 30.00 28.60 27.03 26.25 95 33.04 32.96 32.14 30.95 29.54 27.93 27.10 100 33.94 33.85 33.03 31.85 30.44 28.82 27.98 110 35.55 35.46 34.65 33.49 32.08 30.47 29.62 120 36.97 36.90 36.11 34.98 33.58 31.98 31.14 130 38.28 38.19 37.44 36.33 34.96 33.38 32.55 140 39.44 39.37 38.64 37.56 36.23 34.67 33.85 150 40.49 40.42 39.71 38.67 37.38 35.86 35.04 170 42.21 42.15 41.51 40.54 39.33 37.89 37.11 190 43.62 43.55 42.98 42.10 40.97 39.62 38.90 210 44.77 44.72 44.19 43.40 42.36 41.11 40.42 230 45.71 45.67 45.20 44.48 43.54 42.38 41.74 250 46.48 46.44 46.01 45.38 44.53 43.47 42.87 270 47.11 47.06 46.70 46.13 45.36 44.40 345 43.84 (continued) Chapter 9 346 • Water Influx Table 9.10 Dimensionless Influx, WeD, for rD′ = 10 for Bottomwater Drive (continued) z D′ tD 0.05 0.1 0.3 0.5 0.7 0.9 1.0 290 47.61 47.58 47.25 46.75 46.07 45.19 44.68 310 48.03 48.00 47.72 47.26 46.66 45.87 45.41 330 48.38 48.35 48.10 47.71 47.16 46.45 46.03 350 48.66 48.64 48.42 48.08 47.59 46.95 46.57 400 49.15 49.14 48.99 48.74 48.38 47.89 47.60 450 49.46 49.45 49.35 49.17 48.91 48.55 48.31 500 49.65 49.64 49.58 49.45 49.26 48.98 48.82 600 49.84 49.84 49.81 49.74 49.65 49.50 49.41 700 49.91 49.91 49.90 49.87 49.82 49.74 49.69 800 49.94 49.94 49.93 49.92 49.90 49.85 49.83 900 49.96 49.96 49.94 49.94 49.93 49.91 49.90 1000 49.96 49.96 49.96 49.96 49.94 49.93 49.93 1200 49.96 49.96 49.96 49.96 49.96 49.96 49.96 9.4 Pseudosteady-State Models Theedgewaterandbottomwaterunsteady-statemethodsdiscussedinsection9.3providecorrectproceduresforcalculatingwaterinfluxinnearlyanyreservoirapplication.However,thecalculationstendto besomewhatcumbersome,andthereforetherehavebeenvariousattemptstosimplifythecalculations, includingtheCarter-Tracymodelreferencedearlier.Themostpopularandseeminglyaccuratemethod isonedevelopedbyFetkovich,usinganaquifermaterialbalanceandanequationthatdescribestheflow ratefromtheaquifer.19TheequationsforflowrateusedbyFetkovicharesimilartotheproductivityindexequationdefinedinChapter8.Theproductivityindexrequiredpseudosteady-stateflowconditions. Thusthismethodneglectstheeffectsofthetransientperiodinthecalculationsofwaterinflux,which willobviouslyintroduceerrorsintothecalculations.However,themethodhasbeenfoundtogiveresults similartothoseofthevanEverdingenandHurstmodelinmanyapplications. Fetkovichfirstwroteamaterialbalanceequationontheaquiferforconstantwaterandrock compressibilitiesas p p = − i We + pi W (9.15) where p istheaveragepressureintheaquiferaftertheremovalofWebblofwater,piistheinitial pressureoftheaquifer,andWeiistheinitialencroachablewaterinplaceattheinitialpressure. Fetkovichnextdefinedageneralizedrateequationas 9.4 Pseudosteady-State Models 347 qw Bw = J ( p − pR )ma (9.16) whereqwBwistheflowrateofwaterfromtheaquifer,Jistheproductivityindexoftheaquiferand isafunctionoftheaquifergeometry,pRisthepressureatthereservoir-aquiferboundary,andma is equalto1forDarcyflowduringthepseudosteady-stateflowregion.Equations(9.15)and(9.16) can be combined to yield the following equation (see Fetkovich19 and Dake20 for the complete derivation): Jpi t Wei Wei We = ( pi − pR ) 1 − e pi (9.17) Thisequationwasderivedforconstantpressuresatboththereservoir-aquiferboundary,pR, and theaveragepressureintheaquifer, p. Atthispoint,toapplytheequationtoatypicalreservoir applicationwherebothofthesepressuresarechangingwithtime,itwouldnormallyberequired tousetheprincipleofsuperposition.Fetkovichshowedthatbycalculatingthewaterinfluxfora shorttimeperiod,Δt,withacorrespondingaverageaquiferpressure, p, andanaverageboundary pressure, pR , andthenstartingthecalculationoveragainforanewperiodandnewpressures, superpositionwasnotneeded.Thefollowingequationsareusedinthecalculationforwaterinflux withthismethod: ΔWen = Jp Δ t − i n Wei ( pn −1 − pRn ) 1 − e Wei pi W pn −1 = pi 1 − e Wei pRn = pRn −1 + pRn 2 (9.18) (9.19) (9.20) wherenrepresentsaparticularinterval, pn−1 istheaverageaquiferpressureattheendofthen–1 timeinterval, pRn istheaveragereservoir-aquiferboundarypressureduringintervaln, and We is thetotal,orcumulative,waterinfluxandisgivenby We = ΣΔWen (9.21) Theproductivityindex,J,usedinthecalculationprocedureisafunctionofthegeometryofthe aquifer.Table9.11containsseveralaquiferproductivityindicesaspresentedbyFetkovich.19When youusetheequationsfortheconditionofaconstantpressureouteraquiferboundary,theaverage aquiferpressureinEq.(9.18)willalwaysbeequaltotheinitialouterboundarypressure,whichis usuallypi.Example9.6illustratestheuseoftheFetkovichmethod. Chapter 9 348 Example 9.6 • Water Influx Calculating the Water Influx for the Reservoir in Example 9.4 Using the Fetkovich Approach Given φ=20.9% k=275md(averagereservoirpermeability,presumedthesamefortheaquifer) μ=0.25cp ct = 6 ×10–6 psi–1 h=19.2ft;areaofreservoir=1216ac Estimatedareaofaquifer=250,000ac θ=180° Solution Area ofaquifer = 1 2 250, 000( 43, 560 ) ∂rR or re = 2 0.5π Area of reservoir = 1/2 1 2 1216( 43, 560 ) ∂rR or rR = 2 0.5π = 83, 263 ft 1/2 = 5807 ft θ π (re2 − rR2 )hφ pi ct 360 Wei = 5.615 180 6(10 )−6 π (82, 2632 − 5807 2 )19.2(0.209 )3793 360 Wei = = 176.3(10 )6 bbl 5.615 Table 9.11 Productivity Indices for Radial and Linear Aquifers (Taken from Fetkovich)19 Type of outer aquifer boundary a Radial flowa Finite—noflow θ 0.00708 kh 360 J= i[ln(re / rR ) − 0.75 ] Finite—constantpressure θ 0.00708 kh 360 J= i[ ln(re / rR )] Unitsareinnormalfieldunitswithkinmillidarcies. wiswidthandLislengthoflinearaquifer. b Linear flowb J= 0.00338lkwh iL J= 0.001127 kwh iL 9.4 Pseudosteady-State Models 349 180 θ 0.00708 kh 0.00708(275 )(19.2 ) 360 360 = 39.08 = J= µ[ln(re / rR ) − 0.75 ] 83, 263 − 0.25 ln 0 . 75 5807 Jp Δ t − i n Wei ΔWen = ( pn −1 − pRn ) 1 − e Wei pi 39.08 ( 3793)( 91.3) − 6 176.3(10 6 ) = ( pn −1 − pRn ) 1 − e 176.3(10 ) 3793 39.08 ( 3793)( 91.3) − 6 ΔWen = 3435( pn −1 − pRn ) 1 − e 176.3(10 ) (9.22) ΣΔWen pn −1 = pi 1 − Wei ΣΔWen pn −1 = 3793 1 − 176.3(10 )6 (9.23) SolvingEqs.(9.22)and(9.23),wegetTable9.12. ThewaterinfluxvaluescalculatedbytheFetkovichmethodagreefairlycloselywiththose calculatedbythevanEverdingenandHurstmethodusedinExample9.4.TheFetkovichmethod consistentlygiveswaterinfluxvaluessmallerthanthevaluescalculatedbythevanEverdingenand Table 9.12 Water Influx by Fetkovich Approach Time pR pRn pn−1 − pRn ΔWe We pn 0 3793 3793 0 0 0 3793 1 3788 3790.5 2.5 8,600 8,600 3792.8 2 3774 3781 11.8 40,500 49,100 3791.9 3 3748 3761 30.9 106,100 155,200 3789.7 4 3709 3728.5 61.2 210,000 365,300 3785.1 5 3680 3694.5 90.6 311,200 676,500 3778.4 6 3643 3661.5 116.9 401,600 1,078,100 3769.8 Chapter 9 350 • Water Influx 1,500,000 van Everdingen–Hurst method Fetkovich method Water influx, bbl 1,200,000 900,000 600,000 300,000 0 0 2 4 Quarter 6 8 Figure 9.14 Results of water influx calculations from Example 9.6. Hurstmethodforthisproblem(Fig.9.14).ThisresultcouldbebecausetheFetkovichmethoddoes notapplytoanaquiferthatremainsinthetransienttimeflow.Itisapparentfromobservingthe valuesofpn–1,whicharetheaveragepressurevaluesintheaquifer,thatthepressureintheaquifer isnotdroppingveryfast,whichwouldindicatethattheaquiferisverylargeandthatthewaterflow fromittothereservoircouldbetransientinnature. Problems 9.1 AssumingtheSchilthuissteady-statewaterinfluxmodel,usethepressuredrophistoryfor theConroeFieldgiveninFig.9.15andawaterinfluxconstant,k′,of2170/ft3/day/psitofind thecumulativewaterencroachmentattheendofthesecondandfourthperiodsbygraphical integrationforTable7.1. 9.2 ThepressurehistoryforthePeoriaFieldisgiveninFig.9.16.Between36and48months, productioninthePeoriaFieldremainedsubstantiallyconstantat8450STB/day,atadaily gas-oilratioof1052SCF/STB,and2550STBofwaterperday.TheinitialsolutionGOR was720SCF/STB.ThecumulativeproducedGORat36monthswas830SCF/STB,andat 48months,itwas920SCF/STB.Thetwo-phaseformationvolumefactorat2500psiawas 135 178 225 2044 2748 3434 4179 4916 28 32 36 320 88 1358 16 20 24 Time (t) in months 272 51.5 t 12 0 ∫ (Pi – P)dt 792 351 WE Problems Pressure drop (Pi – P), psi 200 160 120 80 40 0 0 4 8 40 Figure 9.15 Calculation of quantity of water that has encroached into the Conroe Field (after Schilthuis5). 9.050ft3/STB,andthegasvolumefactoratthesamepressurewas0.00490ft3/SCF.Calculatethecumulativewaterinfluxduringthefirst36months. 9.3 Duringaperiodofproductionfromacertainreservoir,theaveragereservoirpressureremainedconstantat3200psia.Duringthestabilizedpressure,theoil-andwater-producing rateswere30,000STB/dayand5000STB/day,respectively.Calculatetheincrementalwater influxforalaterperiodwhenthepressuredropsfrom3000psiato2800psia.Assumethe followingrelationshipforpressureandtimeholds: dp = −0.003 p psi/month dt Otherdataareasfollows: pi=3500psia Rsoi=750SCF/STB Bt=1.45bbl/STBat3200psia Chapter 9 352 • Water Influx 3000 Pressure, psia 2900 2800 2700 2600 2500 2400 0 12 24 36 Time in months 48 60 Figure 9.16 Pressure decline in the Peoria Field. Bg=0.002bbl/STBat3200psia R=800SCF/STBat3200psia Bw=1.04bbl/STBat3200psia 9.4 Thepressuredeclineinareservoirfromtheinitialpressuredowntoacertainpressure,p, wasapproximatelylinearat–0.500psi/day.AssumingtheSchilthuissteady-statewaterinfluxmodelandawaterinfluxconstantofk′,inft3/day-psi,determineanexpressionforthe waterinfluxasafunctionoftimeinbbl. 9.5 Anaquiferof28,850acincludesareservoirof451ac.Theformationhasaporosityof22%, thicknessof60ft,acompressibilityof4(10)–6 psi–1,andapermeabilityof100md.Thewater hasaviscosityof0.30cpandacompressibilityof3(10)–6 psi–1.Theconnatewatersaturation ofthereservoiris26%,andthereservoirisapproximatelycenteredinthisclosedaquifer.It isexposedtowaterinfluxonitsentireperiphery. (a) Calculatetheeffectiveradiioftheaquiferandthereservoirandtheirratio. (b) Calculatethevolumeofwatertheaquifercansupplytothereservoirbyrockcompactionandwaterexpansionperpsiofpressuredropthroughouttheaquifer. (c) Calculatethevolumeoftheinitialhydrocarboncontentsofthereservoir. (d) Calculatethepressuredropthroughouttheaquiferrequiredtosupplywaterequivalent totheinitialhydrocarboncontentsofthereservoir. (e) Calculatethetheoreticaltime-conversionconstantfortheaquifer. (f) CalculatethetheoreticalvalueofB′fortheaquifer. Problems 353 (g) Calculatethewaterinfluxat100days,200days,400days,and800daysifthereservoir boundarypressureisloweredandmaintainedat3450psiafromaninitialpressureof 3500psia. (h) Iftheboundarypressurewaschangedfrom3450psiato3460psiaafter100daysand maintained there, what would the influx be at 200 days, 400 days, and 800 days as measuredfromthefirstpressuredecrementattimezero? (i) Calculatethecumulativewaterinfluxat500daysfromthefollowingboundarypressurehistory: t(days) 0 100 200 300 400 500 p(psia) 3500 3490 3476 3458 3444 3420 (j) Repeatpart(i)assuminganinfiniteaquiferandagainassumingre/rR=5.0. (k) Atwhattimeindaysdotheaquiferlimitsbegintoaffecttheinflux? (l) FromthelimitingvalueofWeDforre/rR=8.0,findthemaximumwaterinfluxavailable perpsidrop.Comparethisresultwiththatcalculatedinpart(b). 9.6 FindthecumulativewaterinfluxforthefifthandsixthperiodsinExample9.4andTable9.3. 9.7 Theactualpressurehistoryofareservoirissimulatedbythefollowingdata,whichassume that the pressure at the original oil-water contact is changed instantaneously by a finite amount,Δp. (a) UsethevanEverdingenandHurstmethodtocalculatethetotalcumulativewater influx. (b) Howmuchofthiswaterinfluxoccurredinthefirst2years? Time in years Δp (psi) 0 40 0.5 60 1.0 94 1.5 186 2.0 110 2.5 120 3.0 Otherreservoirpropertiesincludethefollowing: Reservoirarea=19,600,000ft2 Aquiferarea=686,900,000ft2 Chapter 9 354 • Water Influx k=10.4md φ=25% μw=1.098cp ct=7.01(10)–6 psi–1 h=10ft 9.8 An oil reservoir is located between two intersecting faults as shown in the areal view in Fig.9.17.Thereservoirshownisboundedbyanaquiferestimatedbygeologiststohavean areaof26,400ac.Otheraquiferdataareasfollows: φ=21% k=275md h=30ft ct=7(10)–6 psi–1 μw=0.92cp Theaveragereservoirpressure,measuredat3-monthintervals,isasfollows: Time in days p (psia) 0 2987 91.3 2962 182.6 2927 273.9 2882 365.2 2837 456.5 2793 Aquifer Oil–water contact Fault I Oil reservoir 1350 acres Fault II 60º Figure 9.17 Reservoir between interconnecting faults. Problems 355 Use both the van Everdingen and Hurst and the Fetkovich methods to calculate the waterinfluxthatoccurredduringeachofthe3-monthintervals.Assumethattheaverage reservoirpressurehistoryapproximatestheoilreservoir-aquiferboundarypressurehistory.21 9.9 For the oil reservoir-aquifer boundary pressure relationship that follows, use the van EverdingenandHurstmethodtocalculatethecumulativewaterinfluxateachquarter(see Fig.9.18): φ=20% k=200md h=40ft ct=7(10)–6 psi–1 μw=0.80cp Areaofoilreservoir=1000ac Areaofaquifer=15,000ac 9.10 RepeatProblem9.9usingtheFetkovichmethod,andcomparetheresultswiththeresultsof Problem9.9. 4100 4020 4000 3988 3932 p, psia 3900 3858 3800 3772 3700 3678 3600 0 1 2 3 Quarter Figure 9.18 Boundary pressure relationship for Problem 9.9. 4 5 6 356 Chapter 9 • Water Influx References 1. W. D. Moore and L. G. Truby Jr., “Pressure Performance of Five Fields Completed in a CommonAquifer,”Trans.AlME(1952),195,297. 2. F.M.Stewart,F.H.Callaway,andR.E.Gladfelter,“ComparisonofMethodsforAnalyzinga WaterDriveField,TorchlightTensleepReservoir,Wyoming,”Trans.AlME(1955),204,197. 3. D.HavlenaandA.S.Odeh,“TheMaterialBalanceasanEquationofaStraightLine,”Jour. of Petroleum Technology(Aug.1968),846–900. 4. D.HavlenaandA.S.Odeh,“TheMaterialBalanceasanEquationofaStraightLine:Part II—FieldCases,”Jour. of Petroleum Technology(July1964),815–22. 5. R.J.Schilthuis,“ActiveOilandReservoirEnergy,”Trans.AlME(1936),118,37. 6. S.J.Pirson,Elements of Oil Reservoir Engineering,2nded.,McGraw-Hill,1958,608. 7. A.F.vanEverdingenandW.Hurst,“TheApplicationoftheLaplaceTransformationtoFlow ProblemsinReservoirs,”Trans.AlME(1949),186,305. 8. A.F.vanEverdingen,E.H.Timmerman,andJ.J.McMahon,“ApplicationoftheMaterial BalanceEquationtoaPartialWater-DriveReservoir,”Trans.AlME(1953),198,51. 9. A.T. Chatas, “A PracticalTreatment of Nonsteady-State Flow Problems in Reservoir Systems,”Petroleum Engineering(May1953),25,No.5,B-42;(June1953),No.6,B-38;(Aug. 1953),No.8,B-44. 10. M.J.Edwardsonetal.,“CalculationofFormationTemperatureDisturbancesCausedbyMud Circulation,”Jour. of Petroleum Technology(Apr.1962),416–25. 11. J.R.Fanchi,“AnalyticalRepresentationofthevanEverdingen-HurstInfluenceFunctionsfor ReservoirSimulation,”SPE Jour.(June1985),405–6. 12. M.A.Klins,A.J.Bouchard,andC.L.Cable,“APolynomialApproachtothevanEverdingen-Hurst Dimensionless Variables for Water Encroachment,” SPE Reservoir Engineering (Feb.1988),320–26. 13. R.D.CarterandG.W.Tracy,“AnImprovedMethodforCalculatingWaterInflux,”Trans. AlME(1960),219,415–17. 14. T.Amed,Reservoir Engineering Handbook, 4thed.,Elsevier,2010. 15. I.D.Gates,Basic Reservoir Engineering,KendallHunt,2011. 16. N.Ezekwe,Petroleum Reservoir Engineering Practice,PearsonEducation,2011. 17. K.H.Coats,“AMathematicalModelforWaterMovementaboutBottom-Water-DriveReservoirs,”SPE Jour.(Mar.1962),44–52. 18. D.R.AllardandS.M.Chen,“CalculationofWaterInfluxforBottomwaterDriveReservoirs,” SPE Reservoir Engineering(May1988),369–79. 19. M.J.Fetkovich,“ASimplifiedApproachtoWaterInfluxCalculations—FiniteAquiferSystems,”Jour. of Petroleum Technology(July1971),814–28. 20. L.P.Dake,Fundamentals of Reservoir Engineering,Elsevier,1978. 21. PersonalcontactwithJ.T.Smith. C H A P T E R 1 0 The Displacement of Oil and Gas 10.1 Introduction This chapter includes a discussion of the fundamental concepts that influence the displacement ofoilandgasbothbyinternaldisplacementprocessesandbyexternalfloodingprocesses.Itis meanttobeanintroductiontothesetopicsandnotanexhaustivetreatise.Thereader,ifinterested, isreferredtootherworksthatcoverthematerialinthischapter.1–5Thereservoirengineershould beexposedtotheseconceptsbecausetheyformthebasisforunderstandingsecondaryandtertiary floodingtechniques,discussedinthenextchapter,aswellassomeprimaryrecoverymechanisms. 10.2 Recovery Efficiency TheoverallrecoveryefficiencyEofanyfluiddisplacementprocessisgivenbytheproductof themacroscopic,orvolumetricdisplacement,efficiency,Ev,andthemicroscopicdisplacement efficiency,Ed: E = EvEd (10.1) Themacroscopicdisplacementefficiencyisameasureofhowwellthedisplacingfluidhascontactedtheoil-bearingpartsofthereservoir.Themicroscopicdisplacementefficiencyisameasureof howwellthedisplacingfluidmobilizestheresidualoiloncethefluidhascontactedtheoil. Themacroscopicdisplacementefficiencyismadeupoftwootherterms:theareal,Es, sweep efficiencyandthevertical,Ei,sweepefficiency. 10.2.1 Microscopic Displacement Efficiency Themicroscopicdisplacementefficiencyisaffectedbythefollowingfactors:interfacialandsurfacetensionforces,wettability,capillarypressure,andrelativepermeability. Whenadropofoneimmisciblefluidisimmersedinanotherfluidandcomestorestona solidsurface,thesurfaceareaofthedropwilltakeaminimumvalueowingtotheforcesacting 357 Chapter 10 358 • The Displacement of Oil and Gas atthefluid-fluidandrock-fluidinterfaces.Theforcesperunitlengthactingatthefluid-fluidand rock-fluidinterfacesarereferredtoasinterfacial tensions.Theinterfacialtensionbetweentwofluidsrepresentstheamountofworkrequiredtocreateanewunitofsurfaceareaattheinterface.The interfacialtensioncanalsobethoughtofasameasureoftheimmiscibilityoftwofluids.Typical valuesofoil-brineinterfacialtensionsareontheorderof20dynes/cmto30dynes/cm.Whencertainchemicalagentsareaddedtoanoil-brinesystem,itispossibletoreducetheinterfacialtension byseveralordersofmagnitude. Thetendencyforasolidtopreferonefluidoveranotheriscalledwettability.Wettabilityisa functionofthechemicalcompositionofboththefluidsandtherock.Surfacescanbeeitheroilwet orwaterwet,dependingonthechemicalcompositionofthefluids.Thedegreetowhicharockis eitheroilwetorwaterwetisstronglyaffectedbytheabsorptionordesorptionofconstituentsinthe oilphase.Large,polarcompoundsintheoilphasecanabsorbontothesolidsurface,leavinganoil filmthatmayalterthewettabilityofthesurface. Theconceptofwettabilityleadstoanothersignificantfactorintherecoveryofoil.Thisfactoriscapillary pressure.Toillustratecapillarypressure,consideracapillarytubethatcontainsboth oilandbrine,theoilhavingalowerdensitythanthebrine.Thepressureintheoilphaseimmediatelyabovetheoil-brineinterfaceinthecapillarytubewillbeslightlygreaterthanthepressurein thewaterphasejustbelowtheinterface.Thisdifferenceinpressureiscalledthecapillarypressure, Pc,ofthesystem.Thegreaterpressurewillalwaysoccurinthenonwettingphase.Anexpression relatingthecontactangle,θ;theradius,rc,ofthecapillaryinfeet;theoil-brineinterfacialtension, σwo,indynes/cm;andthecapillarypressureinpsiisgivenby Pc = 9.519(10 )−7 σ wo cos θ rc (10.2) Thisequationsuggeststhatthecapillarypressureinaporousmediumisafunctionofthechemical compositionoftherockandfluids,thepore-sizedistributionofthesandgrainsintherock,and thesaturationofthefluidsinthepores.Capillarypressureshavealsobeenfoundtobeafunction ofthesaturationhistory,althoughthisdependenceisnotreflectedinEq.(10.2).Forthisreason, differentvaluesofcapillarypressureareobtainedduringthedrainageprocess(i.e.,displacingthe wettingphasebythenonwettingphase),thenduringtheimbibitionsprocess(i.e.,displacingthe nonwettingphasewiththewettingphase).Thishysteresisphenomenonisexhibitedinallrockfluidsystems. Ithasbeenshownthatthepressurerequiredtoforceanonwettingphasethroughasmall capillarycanbeverylarge.Forinstance,thepressuredroprequiredtoforceanoildropthrough ataperingconstrictionthathasaforwardradiusof0.00002ft,arearwardradiusof0.00005ft, acontactangleof0°,andaninterfacialtensionof25dynes/cmis0.71psi.Iftheoildropwere 0.00035-ftlong,apressuregradientof2029psi/ftwouldberequiredtomovethedropthroughthe constriction.Pressuregradientsofthismagnitudearenotrealizableinreservoirs.Typicalpressure gradientsobtainedinreservoirsystemsareoftheorderof1psi/ftto2psi/ft. 10.2 Recovery Efficiency 359 Anotherfactoraffectingthemicroscopicdisplacementefficiencyisthefactthatwhentwo ormorefluidphasesarepresentandflowing,thesaturationofonephaseaffectsthepermeability oftheother(s).Thenextsectiondiscussesindetailtheimportantconceptofrelativepermeability. 10.2.2 Relative Permeability Exceptforgasesatlowpressures,thepermeabilityofarockisapropertyoftherockandnotofthe fluidthatflowsthroughit,providedthatthefluidsaturates100%oftheporespaceoftherock.This permeabilityat100%saturationofasinglefluidiscalledtheabsolute permeabilityoftherock. Ifacoresample0.00215ft2incrosssectionand0.1-ftlongflowsa1.0cpbrinewithaformation volumefactorof1.0bbl/STBattherateof0.30STB/dayundera30psipressuredifferential,ithas anabsolutepermeabilityof k= qw Bw μw L 0.30(1.0 )(0.1) = = 413md 0.001127 Ac Δp 0.001127(0.00215 )( 30 ) Ifthewaterisreplacedbyanoilof3.0-cpviscosityand1.2-bbl/STBformationvolumefactor,then, underthesamepressuredifferential,theflowratewillbe0.0834STB/day,andagaintheabsolute permeabilityis k= qo Bo μo L 0.0834 (1.2 )( 3.0 )(0.1) = = 413md 0.001127 Ac Δp 0.001127(0.00215 )( 30 ) Ifthesamecoreismaintainedat70%watersaturation(Sw=70%)and30%oilsaturation (So = 30%), and at these and only these saturations and under the same pressure drop, it flows 0.18STB/dayofthebrineand0.01STB/dayoftheoil,thentheeffectivepermeabilitytowateris kw = qw Bw μw L 0.18(1.0 )(1.0 )(0.1) = = 248 md 0.001127 Ac Δp 0.001127(0.00215 )( 30 ) andtheeffectivepermeabilitytooilis ko = qo Bo μo L 0.01(1.2 )( 3.0 )(0.1) = = 50 md 0.001127 Ac Δp 0.001127(0.00215 )( 30 ) Theeffectivepermeability,then,isthepermeabilityofarocktoaparticularfluidwhenthatfluid hasaporesaturationoflessthan100%.Asnotedintheforegoingexample,thesumoftheeffective permeabilities(i.e.,298md)isalwayslessthantheabsolutepermeability,413md. Whentwofluids,suchasoilandwater,arepresent,theirrelativeratesofflowaredetermined bytheirrelativeviscosities,theirrelativeformationvolumefactors,andtheirrelativepermeabilities. Chapter 10 360 • The Displacement of Oil and Gas Relativepermeabilityistheratioofeffectivepermeabilitytotheabsolutepermeability.Forthepreviousexample,therelativepermeabilitiestowaterandtooilare kw 248 = = 0.60 413 k 50 k = 0.12 kro = o = k 413 krw = The flowing water-oil ratio at reservoir conditions depends on the viscosity ratio and the effectivepermeabilityratio(i.e.,onthemobilityratio),or 0.001127 kw Ac Δp qw Bw μw L k /μ λ = = w w = w =M 0 . 001127 k A Δ p qo Bo λo ko / μ o o c μo L Forthepreviousexample, qw Bw kw / μw 248 / 1.0 = = = 14.9 qo Bo ko / μ o 50 / 3.0 At70%watersaturationand30%oilsaturation,thewaterisflowingat14.9timestheoilrate. Relativepermeabilitiesmaybesubstitutedforeffectivepermeabilitiesinthepreviouscalculation becausetherelativepermeabilityratio,krw/kro,equalstheeffectivepermeabilityratio,kw/ko.The termrelative permeability ratioismorecommonlyused.Forthepreviousexample, krw kw / k kw 248 0.60 = = = = =5 kro ko / k ko 50 0.12 Waterflowsat14.9timestheoilratebecauseofaviscosityratioof3andarelativepermeability ratioof5,bothofwhichfavorthewaterflow.Althoughtherelativepermeabilityratiovarieswith thewater-oilsaturationratio—inthisexample70/30,or2.33—therelationshipisunfortunatelyfar fromoneofsimpleproportionality. Figure10.1showsatypicalplotofoilandwaterrelativepermeabilitycurvesforaparticular rockasafunctionofwatersaturation.Startingat100%watersaturation,thecurvesshowthata decreaseinwatersaturationto85%(a15%increaseinoilsaturation)sharplyreducestherelative permeabilitytowaterfrom100%downto60%,andat15%oilsaturation,therelativepermeability tooilisessentiallyzero.Thisvalueofoilsaturation,15%inthiscase,iscalledthecritical saturation,thesaturationatwhichoilfirstbeginstoflowastheoilsaturationincreases.Itisalsocalled theresidual saturation,thevaluebelowwhichtheoilsaturationcannotbereducedinanoil-water system.Thisexplainswhyoilrecoverybywaterdriveisnot100%efficient.Iftheinitialconnate 10.2 Recovery Efficiency 361 1.0 Relative premeability, KRO and KRW 0.8 0.6 Oil Water 0.4 0.2 0 0 0.2 0.4 0.6 0.8 1.0 Water saturation, fraction of pore space Figure 10.1 Water-oil relative permeability curves. watersaturationis20%forthisparticularrock,thenthemaximumrecoveryfromtheportionofthe reservoirinvadedbyhigh-pressurewaterinfluxis Recovery = Initial − Final 0.80 − 0.15 = = 81% Initial 0.80 Experimentsshowthatessentiallythesamerelativepermeabilitycurvesareobtainedfora gas-watersystemasfortheoil-watersystem,whichalsomeansthatthecritical,orresidual,gas saturationwillbethesame.Furthermore,ithasbeenfoundthatifbothoilandfreegasarepresent, theresidualhydrocarbonsaturation(oilandgas)willbeaboutthesame,inthiscase15%.Suppose,then,thattherockisinvadedbywateratapressurebelowsaturationpressuresothatgashas evolvedfromtheoilphaseandispresentasfreegas.If,forexample,theresidualfreegassaturation behindthefloodfrontis10%,thentheoilsaturationis5%,andneglectingsmallchangesinthe formationvolumefactorsoftheoil,therecoveryisincreasedto Recovery = 0.80 − 0.05 = 94% 0.80 362 Chapter 10 • The Displacement of Oil and Gas Therecovery,ofcourse,wouldnotincludetheamountoffreegasthatoncewaspartoftheinitial oilphaseandhascomeoutofsolution. ReturningtoFig.10.1,asthewatersaturationdecreasesfurther,therelativepermeabilitytowater continuestodecreaseandtherelativepermeabilitytooilincreases.At20%watersaturation,the(connate)waterisimmobile,andtherelativepermeabilitytooilisquitehigh.Thisexplainswhysomerocks maycontainasmuchas50%connatewaterandyetproducewater-freeoil.Mostreservoirrocksare preferentiallywaterwet—thatis,thewaterphaseandnottheoilphaseisnexttothewallsofthepore spaces.Becauseofthis,at20%watersaturation,thewateroccupiestheleast favorableportionsofthe porespaces—thatis,asthinlayersaboutthesandgrains,asthinlayersonthewallsoftheporecavities, andinthesmallercrevicesandcapillaries.Theoil,whichoccupies80%oftheporespace,isinthemost favorableportionsoftheporespaces,whichisindicatedbyarelativepermeabilityof93%.Thecurves furtherindicatethatabout10%oftheporespacescontributenothingtothepermeability,forat10% watersaturation,therelativepermeabilitytooilisessentially100%.Conversely,ontheotherendofthe curves,15%oftheporespacescontribute40%ofthepermeability,foranincreaseinoilsaturationfrom zeroto15%reducestherelativepermeabilitytowaterfrom100%to60%. Indescribingtwo-phaseflowmathematically,itistypicallytherelativepermeabilityratio thatenterstheequations.Figure10.2isaplotoftherelativepermeabilityratioversuswatersaturationforthesamedataofFig.10.1.Becauseofthewiderangeofkro/krwvalues,therelativepermeabilityratioisusuallyplottedonthelogscaleofasemiloggraph.Thecentralormainportionofthe curveisquitelinearonthesemilogplotandinthisportionofthecurve,therelativepermeability ratiomaybeexpressedasafunctionofthewatersaturationby kro = ae− bsw krw (10.3) Theconstantsa and bmaybedeterminedfromthegraphshowninFig.10.2,ortheymaybedeterminedfromsimultaneousequations.AtSw=0.30,kro/krw=25,andatSw=0.70,kro/krw=0.14.Then, 25=ae–0.30band0.14=ae –0.70b Solvingsimultaneously,theintercepta=1220andtheslopeb=13.0.Equation(10.3)indicatesthat therelativepermeabilityratioforarockisafunctionofonlytherelativesaturationsofthefluidspresent.Althoughitistruethattheviscosities,theinterfacialtensions,andotherfactorshavesomeeffect ontherelativepermeabilityratio,foragivenrock,itismainlyafunctionofthefluidsaturations. Inmanyrocks,thereisatransitionzonebetweenthewaterandtheoilzones.Inthetruewater zone,thewatersaturationisessentially100%,althoughinsomereservoirs,asmalloilsaturation maybefoundaconsiderabledistanceverticallybelowtheoil-watercontact.Intheoilzone,thereis usuallyconnatewaterpresent,whichisessentiallyimmobile.Forthepresentexample,theconnate watersaturationis20%andtheoilsaturationis80%.Onlywaterwillbeproducedfromawell completedinthetruewaterzone,andonlyoilwillbeproducedfromthetrueoilzone.Inthetransitionzone(Fig.10.3),bothoilandwaterwillbeproduced,andthefractionthatiswaterwilldepend 10.2 Recovery Efficiency 363 Intercept Kro/Krw = 1222 1000 Slope = 10 2 × 2.303 = 13.0 0.355 2 cycles Relative permeability ratio, Kro /Krw 100 1.0 0.1 ∆SW = 0.355 0.01 0.001 0 0.2 0.4 0.6 0.8 1.0 Water saturation, fraction of pore space Figure 10.2 Semilog plot of relative permeability ratio versus saturation. ontheoilandwatersaturationsatthepointofcompletion.IfthewellinFig.10.3iscompletedin auniformsandatapointwhereSo=60%andSw =40%,thefractionofwaterinreservoirflowrate unitsorreservoirwatercutmaybecalculatedusingEq.(8.19): 0.00708 kw h( pe − pw ) μw ln(re / rw ) 0.00708 ko h( pe − pw ) qo Bo = μo ln(re / rw ) qw Bw = Sincewatercut,fw,isdefinedas fw = qw Bw qw Bw + qo Bo (10.4) Chapter 10 364 Water Water + oil • The Displacement of Oil and Gas Oil Oil Transition zone Water 0 0.2 0.4 0.6 0.8 1.0 Water saturation Figure 10.3 Sketch showing the variation in oil and water saturations in the transition zone. Combiningtheseequationsandcancelingcommonterms, fw = fw = kw / μ w kw / μw + ko /μo 1 1 = ko μ w kro μw 1+ 1+ kw μ o krw μo (10.5) Thefractionalflowinsurfaceflowrateunits,orsurfacewatercut,maybeexpressedas fw′ = 1 kro μw Bw 1+ krw μo Bo (10.6) EitherEq.(10.5)or(10.6)canbeusedwiththedataofFig.10.1andwithviscositydatatocalculate thewatercut.FromFig.10.1,atSw=0.40,krw=0.045,andkro=0.36.Ifμw=1.0cpandμo=3.0cp, thenthereservoirwatercutis 10.2 Recovery Efficiency 365 fw = 1 1 = = 0.27 k μ 0.36(1.0 ) 1 + ro w 1 + krw μo 0.045( 3.0 ) Ifthecalculationsforthereservoirwatercutarerepeatedatseveralwatersaturations,and thenthecalculatedvaluesplottedversuswatersaturation,Fig.10.4willbetheresult.Thisplotis referredtoasthefractional flow curve.Thecurveshowsthatthefractionalflowofwaterranges from0(forSw≤theconnatewatersaturation)to1(forSw ≥ 1minustheresidualoilsaturation). 10.2.3 Macroscopic Displacement Efficiency Thefollowingfactorsaffectthemacroscopicdisplacementefficiency:heterogeneitiesandanisotropy, mobility of the displacing fluids compared with the mobility of the displaced fluids, the physicalarrangementofinjectionandproductionwells,andthetypeofrockmatrixinwhichthe oilorgasexists. 1.0 0.8 fW 0.6 0.4 0.2 0 0 0.2 0.6 0.4 0.8 SW Figure 10.4 Fractional flow curve for the relative permeability data of Figure 10.1. 1.0 366 Chapter 10 • The Displacement of Oil and Gas Heterogeneitiesandanisotropyofahydrocarbon-bearingformationhaveasignificanteffect on the macroscopic displacement efficiency.The movement of fluids through the reservoir will notbeuniformiftherearelargevariationsinsuchpropertiesasporosity,permeability,andclay cement.Limestoneformationsgenerallyhavewidefluctuationsinporosityandpermeability.Also, manyformationshaveasystemofmicrofracturesorlargemacrofractures.Anytimeafractureoccursinareservoir,fluidswilltrytotravelthroughthefracturebecauseofthehighpermeabilityof thefracture,whichmayleadtosubstantialbypassingofhydrocarbon. Manyproducingzonesarevariableinpermeability,bothverticallyandhorizontally,leading toreducedvertical,Ei, and areal, Es,sweepefficiencies.Zonesorstrataofhigherorlowerpermeabilityoftenexhibitlateralcontinuitythroughoutareservoiroraportionthereof.Wheresuch permeabilitystratificationexists,thedisplacingwatersweepsfasterthroughthemorepermeable zonessothatmuchoftheoilinthelesspermeablezonesmustbeproducedoveralongperiodof timeathighwater-oilratios.Thesituationisthesame,whetherthewatercomesfromnaturalinflux orfrominjectionsystems. Thearealsweepefficiencyisalsoaffectedbythetypeofflowgeometryinareservoirsystem. Asanexample,lineardisplacementoccursinuniformbedsofconstantcrosssection,wherethe entireinputandoutflowendsareopentoflow.Undertheseconditions,thefloodfrontadvancesasa plane(neglectinggravitationalforces),andwhenitbreaksthroughattheproducingend,thesweep efficiencyis100%—thatis,100%ofthebedvolumehasbeencontactedbythedisplacingfluid.If thedisplacinganddisplacedfluidsareinjectedintoandproducedfromwellslocatedattheinput andoutflowendsofauniformlinearbed,suchasthedirectline-drivepatternarrangementshown inFig.10.5(a),thefloodfrontisnotaplane,andatbreakthrough,thesweepefficiencyisfarfrom 100%,asshowninFig.10.5(b). Mobilityisarelativemeasureofhoweasilyafluidmovesthroughporousmedia.The apparentmobility,asdefinedinChapter8,istheratioofeffectivepermeabilitytofluidviscosity.Sincetheeffectivepermeabilityisafunctionoffluidsaturations,severalapparentmobilitiescanbedefined.Whenafluidisbeinginjectedintoaporousmediumcontainingboth theinjectedfluidandasecondfluid,theapparentmobilityofthedisplacingphaseisusually measuredattheaveragedisplacingphasesaturationwhenthedisplacingphasejustbeginsto breakthroughattheproductionsite.Theapparentmobilityofthenondisplacingphaseismeasuredatthedisplacingphasesaturationthatoccursjustbeforethebeginningoftheinjection ofthedisplacingphase. Arealsweepefficienciesareastrongfunctionofthemobilityratio.ThemobilityratioM, as definedinChapter8,isameasureoftherelativeapparentmobilitiesinadisplacementprocessand isgivenby M = kw / μ w ko / μ o Aphenomenoncalledviscous fingeringcantakeplaceifthemobilityofthedisplacingphase ismuchgreaterthanthemobilityofthedisplacedphase.Viscousfingeringsimplyreferstothe penetrationofthemuchmoremobiledisplacingphaseintothephasethatisbeingdisplaced. 10.2 Recovery Efficiency 367 Producing well Injection well (a) Figure 10.5(a) Direct-line-drive flooding network. (b) Figure 10.5(b) The photographic history of a direct-line-drive fluid-injection system, under steady-state conditions, as obtained with a blotting-paper electrolytic model (after Wyckoff, Botset, and Muskat6). Figure10.6(b)showstheeffectofmobilityratioonarealsweepefficiencyatinitialbreakthrough forafive-spotnetwork(showninFig.10.6(a))obtainedusingtheX-rayshadowgraph.Thepatternatbreakthroughforamobilityratioof1obtainedwithanelectrolyticmodelisincludedfor comparison. Thearrangementofinjectionandproductionwellsdependsprimarilyonthegeologyof theformationandthesize(arealextent)ofthereservoir.Foragivenreservoir,anoperatorhas theoptionofusingtheexistingwellarrangementordrillingnewwellsinotherlocations.Ifthe operatoroptstousetheexistingwellarrangement,theremaybeaneedtoconsiderconverting productionwellstoinjectionwellsorviceversa.Anoperatorshouldalsorecognizethat,when Chapter 10 368 • The Displacement of Oil and Gas Producing well Injection well (a) Figure 10.6(a) Five-spot flooding network. Mobility ratio = 0.45 Mobility ratio = 1 Mobility ratio = 1.67 X-ray Electrolytic model (b) Figure 10.6(b) X-ray shadowgraph studies showing the effect of mobility ratio on areal sweep efficiency at breakthrough (after Slobod and Caudle7). 10.3 Immiscible Displacement Processes 369 aproductionwellisconvertedtoaninjectionwell,theproductioncapacityofthereservoirwill havebeenreduced.Thisdecisioncanoftenleadtomajorcostitemsinanoverallprojectand shouldbegivenagreatdealofconsideration.Knowledgeofanydirectionalpermeabilityeffects and other heterogeneities can aid in the consideration of well arrangements.The presence of faults,fractures,andhigh-permeabilitystreakscandictatetheshuttinginofawellnearoneof theseheterogeneities.Directionalpermeabilitytrendscanleadtoapoorsweepefficiencyina developedpatternandcansuggestthatthepatternbealteredinonedirectionorthatadifferent patternbeused. Sandstone formations are characterized by a more uniform pore geometry than limestone formations.Limestoneformationshavelargeholes(vugs)andcanhavesignificantfracturesthat areoftenconnected.Limestoneformationsareassociatedwithconnatewaterthatcanhavehigh levelsofdivalentionssuchasCa2+andMg2+.Vugularporosityandhigh-divalentioncontentin theirconnatewatershindertheapplicationofinjectionprocessesinlimestonereservoirs.Onthe otherhand,sometimesasandstoneformationcanbecomposedofsmallsandgrainsthatareso tightlypackedthatfluidswillnotreadilyflowthroughtheformation. 10.3 Immiscible Displacement Processes 10.3.1 The Buckley-Leverett Displacement Mechanism Oilisdisplacedfromarockbywatersimilartohowfluidisdisplacedfromacylinderbyaleaky piston.BuckleyandLeverettdevelopedatheoryofdisplacementbasedontherelativepermeability concept.8Theirtheoryispresentedhere. Consideralinearbedcontainingoilandwater(Fig.10.7).Letthetotalthroughput,q′ = qwBw + qoBo,inreservoirbarrelsbethesameatallcrosssections.Forthepresent,wewillneglectgravitational x O dx q't Water q't AC Oil fw Figure 10.7 Representation of a linear bed containing oil and water. fw – dfw Chapter 10 370 • The Displacement of Oil and Gas andcapillaryforcesthatmaybeacting.LetSwbethewatersaturationinanyelementattimet(days). Thenifoilisbeingdisplacedfromtheelement,attime(t + dt),thewatersaturationwillbe(Sw + dSw). Ifφisthetotalporosityfraction,Acisthecrosssectioninsquarefeet,anddxisthethicknessofthe elementinfeet,thentherateofincreaseofwaterintheelementattimetinbarrelsperdayis dW φ Ac dx ∂Sw = dt 5.615 ∂t x (10.7) Thesubscriptxonthederivativeindicatesthatthisderivativeisdifferentforeachelement.Iffw is thefractionofwaterinthetotalflowof qt′ barrelsperday,then fw qt′ istherateofwaterentering theleft-handfaceoftheelement,dx.Theoilsaturationwillbeslightlyhigherattheright-hand face,sothefractionofwaterflowingtherewillbeslightlyless,orfw – dfw.Thentherateofwater leavingtheelementis ( fw − dfw )qt′. Thenetrateofgainofwaterintheelementatanytime,then,is dW = ( fw − dfw )qt′ − fw qt′ = − qt′dfw dt (10.8) 5.615 qt′ ∂fw ∂Sw = − ∂t x φ Ac ∂x t (10.9) Equating(10.7)and(10.8), Now,foragivenrock,thefractionofwaterfwisafunctiononlyofthewatersaturationSw, as indicatedbyEq.(10.5),assumingconstantoilandwaterviscosities.Thewatersaturation,however,is afunctionofbothtimeandposition,x,whichmaybeexpressedasfw = F(Sw)andSw = G(t, x).Then ∂S ∂f dSw = w dt + w dx ∂t x ∂x t (10.10) Now,thereisinterestindeterminingtherateofadvanceofaconstantsaturationplane,orfront, (∂x/∂t)Sw(i.e.,whereSwisconstant).Then,fromEq.(10.10), (∂Sw / ∂t )x ∂x = − ∂t Sw (∂Sw / ∂x )t (10.11) SubstitutingEq.(10.9)inEq.(10.11), 5.615 qt′ ( ∂fw ∂x )t ∂x = ∂t Sw φ Ac ( ∂Sw ∂x )t (10.12) 10.3 Immiscible Displacement Processes 371 But (∂fw / ∂x )t ∂fw = (∂Sw / ∂x )t ∂Sw t (10.13) 5.615 qt′ ∂fw ∂x = ∂t sw φ Ac ∂Sw t (10.14) Eq.(10.12)thenbecomes Becausetheporosity,area,andthroughputareconstantandbecause,foranyvalueofSw,thederivative∂fw/∂Swisaconstant,theratedx/dtisconstant.Thismeansthatthedistanceaplaneofconstant saturation,Sw,advancesisdirectlyproportionaltotimeandtothevalueofthederivative(∂fw/∂Sw) atthatsaturation,or x= 5.615 qt′t ∂fw φ Ac ∂Sw s (10.15) w WenowapplyEq.(10.15)toareservoirunderactivewaterdrivewherethewallsarelocated inuniformrowsalongthestrikeon40-acspacing,asshowninFig.10.8.Thisgivesrisetoapproximatelinearflow,andifthedailyproductionofeachofthethreewellslocatedalongthedipis200 STBofoilperday,thenforanactivewaterdriveandanoilvolumefactorof1.50bbl/STB,thetotal reservoirthroughput, qt′, willbe900bbl/day. Thecross-sectionalareaistheproductofthewidth,1320ft,andthetrueformationthickness, 20ft,sothatforaporosityof25%,Eq.(10.15)becomes x= 5.615 × 900 × t ∂fw 0.25 × 1320 × 20 ∂Sw s w Ifweletx=0atthebottomofthetransitionzone,asindicatedinFig.10.8,thenthedistancesthe variousconstantwatersaturationplaneswilltravelin,say,60,120,and240daysaregivenby x60 = 46 (∂fw / ∂Sw )sw x120 = 92 (∂fw / ∂Sw )sw x240 = 184 (∂fw / ∂Sw )sw (10.16) Thevalueofthederivative(∂fw/∂Sw)maybeobtainedforanyvalueofwatersaturation,Sw, byplottingfwfromEq.(10.5)versusSwandgraphicallytakingtheslopesatvaluesofSw.Thisis Chapter 10 372 • The Displacement of Oil and Gas 200 200 200 STB/day 40 ac 40 ac 40 ac er at na on c il + w te O x on iti ns ne a Tr zo O er H = 20 ft at 1320 ft W Figure 10.8 Representation of a reservoir under an active water drive. showninFig.10.9at40%watersaturation,usingtherelativepermeabilityratiodataofTable10.1 andawater-oilviscosityratioof0.50.Forexample,atSw=0.40,whereko/kw=5.50(Table10.1), fw = 1 = 0.267 1 + 0.50 × 5.50 TheslopetakengraphicallyatSw=0.40andfw=0.267is2.25,asshowninFig.10.9. Thederivative(∂fw/∂Sw)mayalsobeobtainedmathematicallyusingEq.(10.3)torepresent therelationshipbetweentherelativepermeabilityratioandthewatersaturation.DifferentiatingEq. (10.16),thefollowingisobtained: ∂fw ( μw / μo )bae− bSw ( μw / μo )b( ko / kw ) = = − bSw 2 ∂Sw [1 + ( μw / μo )ae ] [1 + ( μw / μo )( ko / kw )]2 (10.17) Fortheko/kwdataofTable10.1,a=540andb=11.5.Then,atSw=0.40,forexample,byEq.(10.17), ∂fw 0.50 × 11.5 × 5.50 = 2.25 = ∂Sw [1 + 0.50 × 5.50 ]2 10.3 Immiscible Displacement Processes 373 Table 10.1 Buckley-Leverett Frontal Advance Calculations (1) (2) (3) (4) Sw ko kw fw ∂fw ∂Sw μw = 0.50 μo (Eq. [10.5]) (5) ∂fw ∂Sw 46 (6) 92 (7) ∂fw ∂Sw 184 ∂fw ∂Sw (Eq. [10.17]) (60 days; Eq. [10.16]) (120 days; Eq. [10.16]) (240 days; Eq. [10.16]) 0 0 0 0.20 inf. 0.000 0.00 0.30 17.0 0.105 1.08 50 100 200 0.40 5.50 0.267 2.25 104 208 416 0.50 1.70 0.541 2.86 131 262 524 0.60 0.55 0.784 1.95 89 179 358 0.70 0.17 0.922 0.83 38 76 153 0.80 0.0055 0.973 0.30 14 28 55 0.90 0.000 1.000 0.00 0 0 0 100 FW 3.0 dFW dSW 40 2.0 20 1.0 ∆SW = 0.12 0 0 20 30 40 50 60 70 Water saturation, SW , percent Figure 10.9 Watercut plotted versus water saturation. 80 90 Derivative, dFW /dSW 60 dFW 0.27 = = 2.25 dSW 0.12 ∆FW = 0.27 Water cut, FW, percent 80 Chapter 10 374 • The Displacement of Oil and Gas Figure10.9showsthefractionalwatercut,fW,andalsothederivative(∂fw/∂Sw)plottedagainstwater saturationfromthedataofTable10.1.Equation(10.17)wasusedtodeterminethevaluesofthe derivative.SinceEq.(10.3)doesnotholdfortheveryhighandforthequitelowwatersaturation ranges,someerrorisintroducedbelow30%andabove80%watersaturation.Sincetheseareinthe regionsofthelowervaluesofthederivatives,theoveralleffectonthecalculationissmall. ThelowermostcurveofFig.10.10representstheinitialdistributionofwaterandoilinthe linearsandbodyofFig.10.8.Abovethetransitionzone,theconnatewatersaturationisconstantat 20%.Equation(10.16)maybeusedwiththevaluesofthederivatives,calculatedinTable10.1and plottedinFig.10.9,toconstructthefrontal advancecurvesshowninFig.10.10at60,120,and240 days.Forexample,at50%watersaturation,thevalueofthederivativeis2.86;sobyEq.(10.16), at60days,the50%watersaturationplane,orfront,willadvanceadistanceof ∂f x = 46 w = 46 × 2.86 = 131 feet ∂Sw S w This distance is plotted as shown in Fig. 10.10 along with the other distances that have been calculatedinTable10.1fortheothertimevaluesandotherwatersaturations.Thesecurvesarecharacteristicallydoublevaluedortriplevalued.Forexample,Fig.10.10indicatesthatthewatersaturationafter240daysat400ftis20%,36%,and60%.Thesaturationcanbeonlyonevalueatany placeandtime.Thedifficultyisresolvedbydroppingperpendicularssothattheareastotheright (A)equaltheareastotheleft(B),asshowninFig.10.10. 100 Water saturation, percent 80 240 days 60 60 120 131 ft A 40 B 20 Initial water distribution 0 0 100 200 300 400 Distance along bed, feet 500 Figure 10.10 Fluid distributions at initial conditions and at 60, 120, and 240 days. 600 10.3 Immiscible Displacement Processes 100 SOR = 10 percent Unrecoverable oil Recoverable oil after inifinite throughput 80 Water saturation, percent 375 60 Oil recovered after 240 days 40 Gravity Flood front Capillarity 20 Initial water distribution 0 0 100 200 300 400 Distance along bed, feet 500 600 Figure 10.11 Water saturation plotted versus distance along bed. Figure10.11representstheinitialwaterandoildistributionsinthereservoirunitandalso thedistributionsafter240days,providedthefloodfronthasnotreachedthelowermostwell. Theareatotherightoftheflood frontinFig.10.11iscommonlycalledtheoil bankandthe areatotheleftissometimescalledthedrag zone.Theareaabovethe240-daycurveandbelow the90%watersaturationcurverepresentsoilthatmayyetberecoveredordraggedoutofthe high-watersaturationportionofthereservoirbyflowinglargevolumesofwaterthroughit.The areaabovethe90%watersaturationcurverepresentsunrecoverableoil,sincethecriticaloil saturationis10%. This presentation of the displacement mechanism has assumed that capillary and gravitationalforcesarenegligible.Thesetwoforcesaccountfortheinitialdistributionofoilandwater inthereservoirunit,andtheyalsoacttomodifythesharpfloodfrontinthemannerindicatedin Fig.10.11.Ifproductionceasesafter240days,theoil-waterdistributionwillapproachonesimilar totheinitialdistribution,asshownbythedashedcurveinFig.10.11. Figure10.11alsoindicatesthatawellinthisreservoirunitwillproducewater-freeoiluntil thefloodfrontapproachesthewell.Thereafter,inarelativelyshortperiod,thewatercutwillrise sharplyandbefollowedbyarelativelylongperiodofproductionathigh,andincreasinglyhigher, watercuts.Forexample,justbehindthefloodfrontat240days,thewatersaturationrisesfrom20% toabout60%—thatis,thewatercutrisesfromzeroto78.4%(seeTable10.1).Whenaproducing formationconsistsoftwoormoreratherdefinitestrata,orstringers,ofdifferentpermeabilities,the ratesofadvanceintheseparatestratawillbeproportionaltotheirpermeabilities,andtheoverall effectwillbeacombinationofseveralseparatedisplacements,suchasdescribedforasinglehomogeneousstratum. Chapter 10 376 10.3.2 • The Displacement of Oil and Gas The Displacement of Oil by Gas, with and without Gravitational Segregation Themethoddiscussedintheprevioussectionalsoappliestothedisplacementofoilbygasdrive.The treatmentofoildisplacementbygasinthissectionconsidersonlygravitydrainagealongdip.RichardsonandBlackwellshowedthatinsomecasestherecanbeasignificantverticalcomponentofdrainage.9 Duetothehighoil-gasviscosityratiosandthehighgas-oilrelativepermeabilityratiosat lowgassaturations,thedisplacementefficiencybygasisgenerallymuchlowerthanthatbywater,unlessthegasdisplacementisaccompaniedbysubstantialgravitationalsegregation.Thisis basicallythesamereasonforthelowrecoveriesfromreservoirsproducedunderthedissolvedgas drivemechanism.Theeffectofgravitationalsegregationinwater-driveoilreservoirsisusuallyof muchlessconcernbecauseofthehigherdisplacementefficienciesandtheloweroil-waterdensity differences,whereastheconverseisgenerallytrueforgas-oilsystems.Welgeshowedthatcapillary forcesmaygenerallybeneglectedinboth,andheintroducedagravitationalterminEq.(10.5),as willbeshowninthefollowingequations.10Aswithwaterdisplacement,alinearsystemisassumed, andaconstantgaspressurethroughoutthesystemisalsoassumedsothataconstantthroughput ratemaybeused.Theseassumptionsalsoallowustoeliminatechangescausedbygasdensity,oil density,oilvolumefactor,andthelike.Equation(8.1)maybeappliedtoboththeoilandgasflow, assumingtheconnatewaterisessentiallyimmobile,sothatthefractionoftheflowingreservoir fluidvolume,whichisgas,is fg = υg 0.001127 kg − υt μ qυ t dp − 0.00694 ρg cos α dx g (10.18) Thetotalvelocityisvt,whichisthetotalthroughputrate qt′ dividedbythecross-sectionalarea Ac.Thereservoirgasdensity,ρg,isinlbm/ft3.Theconstant0.00694thatappearsinEqs.(10.18) and(10.19)isaresultofmultiplying0.433and62.4lbm/ft3,thedensityofwater.Whencapillary forces are neglected, as they are in this application, the pressure gradients in the oil and gas phasesareequal.Equation(8.1)maybesolvedforthepressuregradientbyapplyingittotheoil phase,or μoυo dp dp + 0.00694 ρo cos α = = − dx o dx g 0.001127 ko (10.19) SubstitutingthepressuregradientofEq.(10.19)inEq.(10.18), fg = − 0.001127 kg μoυo − + 0.00694 ( ρo − ρg ) cos α μ gυ t 0.001127 ko Expandingandmultiplyingthroughby(ko/kg)(μg/μo), (10.20) 10.3 Immiscible Displacement Processes 377 ko μ g υo 7.821(10 −6 )ko ( ρo − ρg ) cos α fg − = μoυt kg μo υt (10.21) Butυo/υtisthefractionofoilflowing,whichequals1minusthegasflowing,(1–fg).Then,finally, 7.821(10 −6 )ko ( ρo − ρg ) cos α 1− μoυt fg = ko μ g 1+ kg μo (10.22) Therelativepermeabilityratio(kro/krg)maybeusedfortheeffectivepermeabilityratiointhedenominator of Eq. (10.22); however, the permeability to oil, ko, in the numerator is the effective permeabilityandcannotbereplacedbytherelativepermeability.Itmay,however,bereplacedwith (krok),wherekistheabsolutepermeability.Thetotalvelocity, υt,isthetotalthroughputrate, qt′, dividedbythecross-sectionalarea,Ac.Insertingtheseequivalents,thefractionalgasflowequation withgravitationalsegregationbecomes 7.821(10 −6 )kAc ( ρo − ρg ) cos α kro 1− μo qt′ fg = ko μ g 1+ kg μo (10.23) Ifthegravitationalforcesaresmall,Eq.(10.23)reducestothesametypeoffractionalflowequationasEq.(10.5),or fg = 1+ 1 ko μ g (10.24) kg μo AlthoughEq.(10.24)isnotratesensitive(i.e.,itdoesnotdependonthethroughputrate), Eq.(10.23)includesthethroughputvelocity qt′ / Ac andisthereforeratesensitive.Sincethetotal throughputrate, qt′, isinthedenominatorofthegravitationaltermofEq.(10.23),rapiddisplacement(i.e.,large [ qt′ / Ac ] )reducesthesizeofthegravitationalterm,andsocausesanincreasein thefractionofgasflowing,fg.Alargevalueoffgimplieslowdisplacementefficiency.Ifthegravitationaltermissufficientlylarge,fgbecomeszero,orevennegative,whichindicatescountercurrent flowofgasupdipandoildowndip,resultinginmaximumdisplacementefficiency.Inthecaseof agascapthatoverliesmostofanoilzone,thedrainageisvertical,andcosα=1.00;inaddition, thecross-sectionalareaislarge.Iftheverticaleffectivepermeabilitykoisnotreducedtoaverylow levelbylowpermeabilitystrata,gravitationaldrainagewillsubstantiallyimproverecovery. Chapter 10 378 • The Displacement of Oil and Gas TheuseofEq.(10.23)isillustratedusingthedatagivenbyWelgefortheMileSixPool,Peru, whereadvantagewastakenofgoodgravitationalsegregationcharacteristicstoimproverecovery.10 Pressuremaintenancebygasinjectionhasbeenpracticedsince1933byreturningproducedgas andothergastothegascapsothatreservoirpressurehasbeenmaintainedwithin200psiofits initialvalue.Figure10.12showstheaveragerelativepermeabilitycharacteristicsoftheMileSix Poolreservoirrock.Asiscommoningas-oilsystems,thesaturationsareexpressedinpercentages ofthehydrocarbonporosity,andtheconnatewater,beingimmobile,isconsideredaspartofthe rock.TheotherpertinentreservoirrockandfluiddataaregiveninTable10.2.Substitutingthese datainEq.(10.25), 7.821(10 −6 )( 300 )(1.237 )(10 6 )( 48.7 − 5 ) cos 72.55° kro 1− 1.32 11, 600 fg = k (0.0134 ) 1+ o kg (1.32 ) fg = 1 − 2.50 kro k 1 + 0.0102 o kg (10.25) ThevaluesoffghavebeencalculatedinTable10.2forthreeconditions:(1)assumingnegligible gravitational segregation by using Eq. (10.24); (2) using the gravitational term equal to 2.50 krofortheMileSixPool,Eq.(10.25);and(3)assumingthegravitationaltermequals1.25kro, orhalfthevalueatMileSixPool.Thevaluesoffgforthesethreeconditionsareshownplottedin Fig.10.13.ThenegativevaluesoffgfortheconditionsthatexistedintheMileSixPoolindicate countercurrentgasflow(i.e.,gasupdipandoildowndip)intherangeofgassaturationsbetweenan assumedcriticalgassaturationof5%andabout17%. ThedistanceofadvanceofanygassaturationplanemaybecalculatedfortheMileSixPool, usingEq.(10.15),replacingwaterasthedisplacingfluidbygas,or x= 5.615 qt′t ∂fg φ Ac ∂Sg Sg In100days,then, x= 5.615(11, 600 )(100 ) ∂fg 0.1625(1, 237, 000 ) ∂Sg ∂fg x = 32.4 ∂Sg S Sg (10.26) g 10.3 Immiscible Displacement Processes 379 1.0 Relative permeabilities 0.8 0.6 KG KO 0.4 0.2 0 1.0 0.8 0.6 0.4 0.2 Gas saturation, fraction of hydrocarbon pore space 0 Figure 10.12 Relative permeabilities for the Mile Six Pool, Peru. 1.0 No gravity Tangent at SG = 0.10 Fraction of gas in stream, FG 0.8 Gravity term = 1.25 KRO Tangent at SG = 0.18 in rig 0.6 o rom Gravity term = 2.50 KRO Tangent at SG = 0.40 nt f a Sec 0.4 0.2 0 Countercurrent gas flow–negative FG –0.2 –0.4 0 Figure 10.13 0.1 0.2 0.3 0.4 Gas saturation, SG, fraction Fraction of gas in reservoir stream for the Mile Six Pool, Peru. 0.5 0.6 Table 10.2 Mile Six Pool Reservoir Data and Calculations Averageabsolutepermeability=300md Reservoiroilspecificgravity=0.78(water=1) Averagehydrocarbonporosity=0.1625 Reservoirgasspecificgravity=0.08(water=1) Averageconnatewater=0.35 Reservoirtemperature=114°F Averagedipangle=17°30′(α=90°–17°30′) Averagereservoirpressure=850psia Averagecross-sectionalarea=1,237,000sqft Averagethroughput=11,600reservoirbblperday Reservoiroilviscosity=1.32cp Oilvolumefactor=1.25bbl/STB Reservoirgasviscosity=0.0134cp Solutiongasat850psia=400SCF/STB Gasdeviationfactor=0.74 Sg 0.05 0.10 0.15 0.20 0.25 0.30 0.35 0.40 0.45 0.50 0.55 0.60 ko/kg inf. 38 8.80 3.10 1.40 0.72 0.364 0.210 0.118 0.072 0.024 0.00 0.993 0.996 0.998 0.990 1.00 1.00 1.00 Gravity term = 0 0.720 0.918 0.969 0.986 ∂fg/∂Sg 7.40 1.20 0.60 0.30 x=32∂fg/∂Sg 237 38 19 10 fg 0 Gravity term = 2.50 × kro kro 0.77 0.59 0.44 0.34 0.26 0.19 0.14 0.10 0.065 0.040 0.018 0.00 2.50× kro 1.92 1.48 1.10 0.85 0.65 0.48 0.35 0.25 0.160 0.10 0.045 0.00 1–2.5kro –0.92 –0.48 –0.10 0.15 0.35 0.52 0.65 0.75 0.84 0.90 0.955 1.00 fg 0 1.00 –0.29 –0.092 0.145 0.345 0.516 0.647 0.749 0.840 0.900 0.955 ∂fg/∂Sg 3.30 4.40 4.30 3.60 3.00 2.50 1.95 1.60 1.20 0.80 32∂fg/∂Sg 106 141 138 115 96 80 62 51 38 26 Gravity term = 1.25 × kro 1.25kro 0.96 0.74 0.55 0.425 0.325 0.240 0.175 0.125 0.080 0.050 0.023 0.00 1–1.25kro 0.04 0.26 0.45 0.575 0.675 0.760 0.825 0.875 0.920 0.950 0.977 1.00 fg 0.190 0.413 0.557 0.666 0.755 0.822 0.873 0.920 0.950 0.977 1.00 ∂fg/∂Sg 4.00 3.60 2.40 1.90 1.50 1.20 1.00 0.80 0.60 32∂fg/∂Sg 128 115 77 61 48 38 32 26 19 10.3 Immiscible Displacement Processes 381 Thevaluesofthederivatives(∂fg/∂Sg)giveninTable10.2havebeendeterminedgraphically fromFig.10.13.Figure10.14showstheplotsofEq.(10.26)toobtainthegas-oildistributionsand thepositionsofthegasfrontafter100days.Theshapeofthecurveswillnotbealteredforanyothertime.Thedistributionandfrontsat1000days,forexample,maybeobtainedbysimplychanging thescaleonthedistanceaxisbyafactorof10. Welgeshowedthatthepositionofthefrontmaybeobtainedbydrawingasecantfromthe originasshowninFig.10.13.10Forexample,thesecantistangenttothelowercurveat40%gas saturation.Then,inFig.10.14,thefrontmaybefoundbydroppingaperpendicularfromthe 40%gassaturationasindicated.ThiswillbalancetheareasoftheS-shapedcurve,whichwas donebytrialanderrorinFig.10.10forwaterdisplacement.Inthecaseofwaterdisplacement, thesecantshouldbedrawn,notfromtheorigin,butfromtheconnatewatersaturation,asindicatedbythedashedlineinFig.10.9.Thisistangentatawatersaturationof60%.Referringto Fig.10.10,the240-dayfrontisseentooccurat60%watersaturation.Owingtothepresence ofaninitialtransitionzone,thefrontsat60daysand120daysoccuratslightlylowervaluesof watersaturation. Themuchgreaterdisplacementefficiencywithgravitysegregationthanwithoutisapparent fromFig.10.14.Sincethepermeabilitytooilisessentiallyzeroat60%gassaturation,themaximumrecoverybygasdisplacementandgravitydrainageis60%oftheinitialoilinplace.Actually, somesmallpermeabilitytooilexistsatevenverylowoilsaturations,whichexplainswhysome fields may continue to produce at low rates for quite long periods after the pressure has been depleted.ThedisplacementefficiencymaybecalculatedfromFig.10.14bythemeasurementof 1.0 Unrecoverable oil KRO = 0 at SG = 0.6 Saturation 0.8 0.6 A Gravity term = 2.5 KRO Secant tangent at SG = 0.4 0.4 Gravity term = 1.25 KRO B Secant tangent at SG = 0.18 0.2 No gravity Secant tangent at SG = 0.1 0 0 40 80 120 160 Distance in 100 days, feet 200 Figure 10.14 Fluid distributions in the Mile Six Pool after 100 days injection. 240 Chapter 10 382 • The Displacement of Oil and Gas areas.Forexample,thedisplacementefficiencyatMileSixPoolwithfullgravitysegregationisin excessof Recovery = Area B 32.5 = = 0.874, or 87.4% Area A + Area B 4.7 + 32.5 Ifthegravitysegregationhadbeenhalfaseffective,therecoverywouldhavebeenabout60%; without gravity segregation, the recovery would have been only 24%.These recoveries are expressedaspercentagesoftherecoverable oil.Intermsoftheinitial oilinplace,therecoveriesare only60%aslarge,or52.4%,36.0%,and14.4%,respectively.Welge,ShreveandWelch,Kern, andothershaveextendedtheconceptspresentedheretothepredictionofgas-oilratios,productionrates,andcumulativerecoveries,includingthetreatmentofproductionfromwellsbehindthe displacementfront.10,11,12Smithhasusedthemagnitudeofthegravityterm[(ko/μo)(ρo – ρg)cosα] asacriterionfordeterminingthosereservoirsinwhichgravitysegregationislikelytobeofconsiderableimportance.13ThedataofTable10.3indicatethatthisgravitytermmusthaveavalueabove about600intheunitsusedtobeeffective.AninspectionofEq.(10.23),however,showsthatthe throughputvelocity ( qt′ / Ac ) isalsoofprimaryimportance. Oneinterestingapplicationofgravitysegregationistotherecoveryofupdipor“attic”oilin activewater-drivereservoirspossessinggoodgravitysegregationcharacteristics.Whenthestructurallyhighestwell(s)hasgonetowaterproduction,high-pressuregasisinjectedforaperiod.This gasmigratesupdipanddisplacestheoildowndip,whereitmaybeproducedfromthesamewellin whichthegaswasinjected.Theinjectedgasis,ofcourse,unrecoverable. Itappearsfromthepreviousdiscussionsandexamplesthatwaterisgenerallymoreefficient thangasindisplacingoilfromreservoirrocks,mainlybecause(1)thewaterviscosityisoftheorderof50timesthegasviscosityand(2)thewateroccupiesthelessconductiveportionsofthepore spaces,whereasthegasoccupiesthemoreconductiveportions.Thus,inwaterdisplacement,the oilislefttothecentralandmoreconductiveportionsoftheporechannels,whereasingasdisplacement,thegasinvadesandoccupiesthemoreconductiveportionsfirst,leavingtheoilandwaterto thelessconductiveportions.Whathasbeensaidofwaterdisplacementistrueforpreferentially water wet(hydrophilic)rock,whichisthecaseformostreservoirrocks.Whentherockispreferentiallyoil wet(hydrophobic),thedisplacingwaterwillinvadethemoreconductiveportionsfirst, justasgasdoes,resultinginlowerdisplacementefficiencies.Inthiscase,theefficiencybywater stillexceedsthatbygasbecauseoftheviscosityadvantagethatwaterhasovergas. 10.3.3 Oil Recovery by Internal Gas Drive Oilisproducedfromvolumetric,undersaturatedreservoirsbyexpansionofthereservoirfluids. Downtothebubble-pointpressure,theproductioniscausedbyliquid(oilandconnatewater)expansionandrockcompressibility(seeChapter6,section6.6).Belowthebubblepoint,theexpansionoftheconnatewaterandtherockcompressibilityarenegligible,andastheoilphasecontracts owingtoreleaseofgasfromsolution,productionisaresultofexpansionofthegasphase.When Table 10.3 Gravity Drainage Experience (after R. H. Smith, Except for Mile Six Pool13) Field and reservoir Lakeview Dip angle (deg.) cos αa Density difference, Δp Gravity drainage term, ko Δρ cos α μo Sand thickness (ft) Gravity drainage 17 2000 118 24 0.41 53.7 2590 100 Yes 383 LanceCreek 27B 0.4 80 200 4.5 0.08 39.3 630 Thin bedding Yes SunDance E2–3 1.3 1100 846 22 0.37 40.6 12,710 45 Yes OklahomaCity 2.1 600 286 36 0.59 34.9 5880 ? Yes Kettleman,Temblor 0.8 72 90 30 0.50 35.6 1600 80 Yes WestCoyote,Emery 1.45 28 19.3 17 0.29 38.1 210 75 ? SanMiguelito,First Grubb 1.1 34 30.9 39 0.62 39.3 750 40 Yes HuntingtonBeach, LowerAshton 1.8 125 69 25 0.42 41.8 1220 50 Yes Ellwood,Vaqueros 1.5 250 167 32 0.53 43.1 3810 120 Yes SanArdo,Campbell 2000 4700 2.35 4 0.07 56.2 10 230 ... Wilmington,Upper TerminalBlockV 12.6 284 22.5 4 0.07 52.4 80 40 ... 40 600 15 11 0.19 54.3 150 40 No 1.32 300 224 17.5 0.30 43.7 2980 635 Yes HuntingtonBeach,Jones MileSixPool,Peru a Oil Oil Oil viscosity permeability mobility (cp) (md) (md/cp) α=90°– dip angle 384 Chapter 10 • The Displacement of Oil and Gas thegassaturationreachesthecriticalvalue,freegasbeginstoflow.Atfairlylowgassaturations, thegasmobility,kg/μg,becomeslarge,andtheoilmobility,ko/μo,becomessmall,resultinginhigh gas-oilratiosandinlowoilrecoveries,usuallyintherangeof5%to25%. Becausethegasoriginatesinternallywithintheoil,themethoddescribedintheprevious sectionforthedisplacementofoilbyexternalgasdriveisnotapplicable.Inaddition,constant pressurewasassumedintheexternaldisplacementsothatthegasandoilviscositiesandvolume factorsremainedconstantduringthedisplacement.Withinternalgasdrive,thepressuredropsas productionproceeds,andthegasandoilviscositiesandvolumefactorscontinuallychange,further complicatingthemechanism. Becauseofthecomplexityoftheinternalgasdrivemechanism,anumberofsimplifyingassumptionsmustbemadetokeepthemathematicalformsreasonablysimple.Thefollowingassumptions,generallymade,doreducetheaccuracyofthemethodsbut,inmostcases,notappreciably: 1. Uniformityofthereservoiratalltimesregardingporosity,fluidsaturations,andrelativepermeabilities.Studieshaveshownthatthegasandoilsaturationsaboutwellsaresurprisingly uniformatallstagesofdepletion. 2. Uniform pressure throughout the reservoir in both the gas and oil zones. This means the gasandoilvolumefactors,thegasandoilviscosities,andthesolutiongaswillbethesame throughoutthereservoir. 3. Negligiblegravitysegregationforces 4. Equilibriumatalltimesbetweenthegasandtheoilphases 5. Agasliberationmechanismthatisthesameasthatusedtodeterminethefluidproperties 6. Nowaterencroachmentandnegligiblewaterproduction Severalmethodsappearintheliteratureforpredictingtheperformanceofinternalgasdrive reservoirsfromtheirrockandfluidproperties.Threearediscussedinthischapter:(1)Muskat’s method,(2)Schilthuis’smethod,and(3)Tarner’smethod.14,15,16Thesemethodsrelatethepressure declinetotheoilrecoveryandthegas-oilratio. The reader will recall that the material balance is successful in predicting the performanceofvolumetricreservoirsdowntopressuresatwhichfreegasbeginstoflow.Inthestudy of the Kelly-Snyder Field, Canyon Reef Reservoir, for example, in Chapter 6, section 6.4, theproducedgas-oilratiowasassumedtobeequaltothedissolvedgas-oilratio,downtothe pressureatwhichthegassaturationreached10%,thecriticalgassaturationassumedforthat reservoir.Belowthispressure(i.e.,athighergassaturations),bothgasandoilflowtothewellbores, their relative rates being controlled by their viscosities, which change with pressure, andbytheirrelativepermeabilities,whichchangewiththeirsaturations.Itisnotsurprising, then,thatthematerialbalanceprinciple(static)iscombinedwiththeproducinggas-oilratio equation(dynamic)topredicttheperformanceatpressuresatwhichthegassaturationexceeds thecriticalvalue. IntheMuskatmethod,thevaluesofthemanyvariablesthataffecttheproductionofgasand oilandthevaluesoftheratesofchangesofthesevariableswithpressureareevaluatedatanystage 10.3 Immiscible Displacement Processes 385 ofdepletion(pressure).Assumingthesevaluesholdforasmalldropinpressure,theincremental gasandoilproductioncanbecalculatedforthesmallpressuredrop.Thesevariablesarerecalculatedatthelowerpressure,andtheprocessiscontinuedtoanydesiredabandonmentpressure.To derivetheMuskatequation,letVpbethereservoirporevolumeinbarrels.Then,thestock-tank barrelsofoilremaining Nratanypressurearegivenby Nr = SoVp Bo =stock-tankbarrels (10.27) Differentiatingwithrespecttopressure, 1 dSo So dBo dN r = Vp − dp Bo dp Bo2 dp (10.28) Thegasremaininginthereservoir,bothfreeanddissolved,atthesamepressure,instandardcubic feet,is Gr = RsoVp So Bo + (1 − So − Sw )Vp Bg (10.29) Differentiatingwithrespecttopressure, R dS dGr S dRso Rso So dBo (1 − So − Sw ) dBg 1 dSo = Vp so o + o − − − 2 2 dp dp Bg dp Bo dp Bg Bo dp Bo dp (10.30) Ifreservoirpressureisdroppingattheratedp/dt,thenthecurrentorproducinggas-oilratioatthis pressureis R= dGr / dp dN r / dp (10.31) SubstitutingEqs.(10.28)and(10.30)inEq.(10.31), 1 dSo Rso dSo So dRso Rso so dBo (1 − So − Sw ) dBg + − 2 − − Bo dp Bo dp dp Bg dp Bo dp Bg2 R= 1 dSo So dBo − Bo dp Bo2 dp (10.32) Chapter 10 386 • The Displacement of Oil and Gas Equation(10.32)issimplyanexpressionofthematerialbalanceforvolumetric,undersaturated reservoirsindifferentialform.Theproducinggas-oilratiomayalsobewrittenas R = Rso + kg μo Bo ko μg Bg (10.33) Equation(10.33)appliesbothtotheflowingfreegasandtothesolutiongasthatflowstothewellboreintheoil.Thesetwotypesofgasmakeupthetotalsurfaceproducinggas-oilratio,R,inSCF/ STB.Equation(10.33)maybeequatedtoEq.(10.32)andsolvedfordSo/dptogive So Bg dRso So kg μo dBo (1 − So − Sw ) dBg + − Bo dp Bo ko μ g dp Bg dp dSo = k dp g μo 1+ ko μ g (10.34) TosimplifythehandlingofEq.(10.34),thetermsinthenumeratorthatarefunctionsofpressure mayonlybegroupedtogetherandgiventhegroupsymbolsX(p),Y(p),andZ(p)asfollows: X ( p) = Bg dRso 1 μo dBo 1 dBg ; Y ( p) = ; Z ( p) = Bo dp Bo μ g dp Bg dp (10.35) UsingthesegroupsymbolsandplacingEq.(10.34)inanincrementalform, kg So X ( p ) + So Y ( p ) − (1 − So − Sw )Z ( p ) ko ΔSo = Δp kg μo 1+ k μ o g (10.36) Equation(10.36)givesthechangeinoilsaturationthataccompaniesapressuredrop,Δp.ThefunctionsX(p),Y(p),andZ(p)areobtainedfromthereservoirfluidpropertiesusingEq.(10.35).The valuesofthederivativesdRso/dp, dBo/dp, and dBg/dparefoundgraphicallyfromtheplotsofRso, Bo, and Bg versuspressure.IthasbeenfoundthatwhendeterminingdBg/dp,thenumbersaremore accuratelyobtainedbyplotting1/Bgversuspressure.Whenthisisdone,thefollowingsubstitution isused: d (1 / Bg ) dp dBg dp =− = − Bg2 1 dBg Bg2 dp d (1 / Bg ) dp 10.3 Immiscible Displacement Processes 387 or Z ( p) = d (1 / Bg ) 1 2 d (1 / Bg ) − Bg = − Bg Bg dp dp (10.37) IncalculatingΔSoforanypressuredropΔp,thevaluesofSo, X(p),Y(p),Z(p),kg/ko, and μo/μg atthebeginningoftheintervalmaybeused.Betterresultswillbeobtained,however,ifvaluesat themiddleofthepressuredropintervalareused.ThevalueofSoatthemiddleoftheintervalcan becloselyestimatedfromtheΔSovalueforthepreviousintervalandthevalueofkg/kousedcorrespondingtotheestimatedmidintervalvalueoftheoilsaturation.InadditiontoEq.(10.36),the totaloilsaturationmustbecalculated.ThisisdonebysimplymultiplyingthevalueofΔSo/Δpby thepressuredrop,Δp,andthensubtractingtheΔSofromtheoilsaturationvaluethatcorresponds tothepressureatthebeginningofthepressuredropinterval,asshowninthefollowingequation: ΔS Soj = So( j −1) − Δp o Δp (10.38) wherejcorrespondstothepressureattheendofthepressureincrementandj–1correspondsto thepressureatthebeginningofthepressureincrement. ThefollowingprocedureisusedtosolvefortheΔSoforagivenpressuredropΔp: 1. PlotRso, Bo, and Bgor1/Bgversuspressureanddeterminetheslopeofeachplot. 2. SolveEq.(10.36)forΔSo/Δpusingtheoilsaturationthatcorrespondstotheinitialpressure ofthegivenΔp. 3. EstimateSojusingEq.(10.38). 4. SolveEq.(10.36)usingtheoilsaturationfromstep3. 5. DetermineanaveragevalueforΔSo/Δpfromthetwovaluescalculatedinsteps2and4. 6. Using(ΔSo/Δp)ave,solveforSojusingEq.(10.38).ThisvalueofSojbecomesSo(j–1)forthenext pressuredropinterval. 7. Repeatsteps2through6forallpressuredropsofinterest. TheSchilthuismethodbeginswiththegeneralmaterialbalanceequation,whichreducesto thefollowingforavolumetric,undersaturatedreservoir,usingthesingle-phaseformationvolume factor: N= N p [ Bo + Bg ( Rp − Rso )] Bo − Boi + Bg ( Rsoi − Rso ) (10.39) Noticethatthisequationcontainsvariablesthatareafunctionofonlythereservoirpressure,Bt, Bg, Rsoi, and Bti,andtheunknownvariables,Rp and Np. Rp,ofcourse,istheratioofcumulativeoil Chapter 10 388 • The Displacement of Oil and Gas production,Np,tocumulativegasproduction,Gp.TousethisequationasapredictivetoolforNp, a methodmustbedevelopedtoestimateRp.TheSchilthuismethodusesthetotalsurfaceproducing gas-oilratioortheinstantaneousgas-oilratio,R,definedpreviouslyinEq.(10.33)as R = Rso + kg μo Bo ko μg Bg (10.33) Thefirsttermontheright-handsideofEq.(10.33)accountsfortheproductionofsolution gas,andthesecondtermaccountsfortheproductionoffreegasinthereservoir.Thesecondterm isaratioofthegastooilflowequationsdiscussedinChapter8.TocalculateRwithEq.(10.33), informationaboutthepermeabilitiestogasandoilisrequired.Thisinformationisusuallyknown fromlaboratorymeasurementsasafunctionoffluidsaturationsandisoftenavailableingraphic form(seeFig.10.15).Thefluidsaturationequationisalsoneeded: N p Bo SL = Sw + (1 − Sw ) 1 − N Boi (10.40) where SL is the total liquid saturation (i.e., SL = Sw + So, which also equals 1 – Sg). Thesolutionofthissetofequationstoobtainproductionvaluesrequiresatrial-and-error procedure.First,thematerialbalanceequationisrearrangedtoyieldthefollowing: Np [ Bo + Bg ( Rp − Rso )] N −1 = 0 Bo − Boi + Bg ( Rsoi − Rso ) (10.41) AlltheparametersinEq.(10.41)areknownasfunctionsofpressurefromlaboratorystudies exceptNp/N and Rp.WhenthecorrectvaluesofthesetwovariablesareusedinEq.(10.41)ata givenpressure,thentheleft-handsideoftheequationequalszero.Thetrial-and-errorprocedure followsthissequenceofsteps: 1. Guessavalueforanincrementaloilproduction(ΔNp/N)thatoccursduringasmalldropin theaveragereservoirpressure(Δp). 2. Determinethecumulativeoilproductiontopressurepj = pj–1 – Δpbyaddingalltheprevious incrementaloilproductionstotheguessduringthecurrentpressuredrop.Thesubscript,j–1, referstotheconditionsatthebeginningofthepressuredropandjtotheconditionsattheend ofthepressuredrop. 10.3 Immiscible Displacement Processes 389 kg ko Fluid saturation Figure 10.15 Permeability ratio versus fluid saturation. Np N =∑ ΔN p (10.42) N 3. Solvethetotalliquidsaturationequation,Eq.(10.40),forSLatthecurrentpressureofinterest. 4. KnowingSL,determineavalueforkg/kofrompermeabilityratioversussaturationinformation,andthensolveEq.(10.33)forRjatthecurrentpressure. 5. Calculatetheincrementalgasproductionusinganaveragevalueofthegas-oilratiooverthe currentpressuredrop: Rave = ΔG p N = R j −1 + R j 2 ΔN p N ( Rave ) (10.43) (10.44) 6. Determinethecumulativegasproductionbyaddingallpreviousincrementalgasproductions inasimilarmannertostep2,inwhichthecumulativeoilwasdetermined. Gp N =∑ ΔG p N (10.45) Chapter 10 390 • The Displacement of Oil and Gas 7. CalculateavalueforRpwiththecumulativeoilandgasamounts. Rp = Gp / N Np / N (10.46) 8. Withthecumulativeoilrecoveryfromstep2andtheRpfromstep7,solveEq.(10.41)to determineiftheleft-handsideequalszero.Iftheleft-handsidedoesnotequalzero,thena newincrementalrecoveryshouldbeguessedandtheprocedurerepeateduntilEq.(10.41)is satisfied. Anyoneofanumberofiterationtechniquescanbeusedtoassistinthetrial-and-errorprocedure.Onethathasbeenusedisthesecantmethod,17whichhasthefollowingiterationformula: x − xn −1 xn+1 = xn − fn n fn − fn −1 (10.47) To apply the secant method to the foregoing procedure, the left-hand side of Eq. (10.41) becomesthefunction,f,andthecumulativeoilrecoverybecomesx.Thesecantmethodprovides thenewguessforoilrecovery,andthesequenceofstepsisrepeateduntilthefunction,f,iszeroor withinaspecifiedtolerance(e.g.,±10–4).Thesolutionproceduredescribedearlierisfairlyeasyto programonacomputer.TheauthorsarekeenlyawarethatprogramslikeExcelcanbeusedtosolve thisproblemwithoutwritingaseparateprogramtoincludeasolutionprocedurelikethesecant method.However,anunderstandingofthesecantmethodmayhelpthereadertovisualizehow thesesolverswork,andforthatreason,itispresentedhere. TheTarnermethodforpredictingreservoirperformancebyinternalgasdriveispresented inaformproposedbyTracy.18Neglectingtheformationandwatercompressibilityterms,thegeneralmaterialbalanceintermsofthesingle-phaseoilformationvolumefactormaybewrittenas follows: N= N p [ Bo − Rso Bg ] + G p Bg − (We − W p ) mBoi Bo − Boi + ( Rsoi − Rso ) Bg + + ( Bg − Bgi ) Bgi (10.48) Tracysuggestedwriting Φn = Bo − Boi + ( Rsoi Bo − Rso Bg mBoi − Rso ) Bg + + ( Bg − Bgi ) Bgi (10.49) 10.3 Immiscible Displacement Processes Φg = Φw = 391 Bg Bo − Boi + ( Rsoi − Rso ) Bg + mBoi + ( Bg − Bgi ) Bgi 1 Bo − Boi + ( Rsoi − Rso ) Bg + mBoi + ( Bg − Bgi ) Bgi (10.50) (10.51) whereΦn, Φg, and Φwaresimplyaconvenientcollectionofmanyterms,allofwhicharefunctions of pressure, except the ratio m, the initial free gas-to-oil volume.The general material balance equationmaynowbewrittenas N = NpΦn + GpΦg–(We –Wp)Φw (10.52) Applyingthisequationtothecaseofavolumetric,undersaturatedreservoir, N = NpΦn + GpΦg (10.53) In progressing from the conditions at any pressure, pj–1, to a lower pressure, pj,Tracy suggested the estimation of the producing gas-oil ratio,R, at the lower pressure rather than estimating the production ΔNp during the interval, as we did in the Schilthuis method. The valueofRmaybeestimatedbyextrapolatingtheplotofRversuspressure,ascalculatedatthe higherpressure.Thentheestimatedaveragegas-oilratiobetweenthetwopressuresisgiven byEq.(10.43): Rave = R j −1 + R j 2 (10.43) Fromthisestimatedaveragegas-oilratiofortheΔpinterval,theestimatedproduction,ΔNp,forthe intervalismadeusingEq.(10.53)inthefollowingform: N=(Np(j–1) + ΔNp)Φnj+(Gp(j–1)+ Rave(ΔNp))Φgj (10.54) FromthevalueofΔNpinEq.(10.56),thevalueofNpjisfound: Npj = Np(j–1) + ΔNp (10.55) In addition to these equations, the total liquid saturation equation is required, Eq. (10.40).The solutionprocedurebecomesasfollows: Chapter 10 392 • The Displacement of Oil and Gas 1. CalculatethevaluesofΦn and Φgasafunctionofpressure. 2. EstimateavalueforRjinordertocalculateanRaveforapressuredropofinterest,Δp. 3. CalculateΔNpbyrearrangingEq.(10.54)togive ΔN p = N − N p( j −1) Φ n − G p( j −1) Φ g (10.56) Φ n + Φ g Rave 4. CalculatethetotaloilrecoveryfromEq.(10.55). 5. Determinekg/kobycalculatingthetotalliquidsaturation,SL,fromEq.(10.40)andusingkg/ko versussaturationinformation. 6. CalculateavalueofRjbyusingEq.(10.33),andcompareitwiththeassumedvalueinstep 2.Ifthesetwovaluesagreewithinsometolerance,thentheΔNpcalculatedinstep3iscorrectforthispressuredropinterval.IfthevalueofRjdoesnotagreewiththeassumedvalue instep2,thenthecalculatedvalueshouldbeusedasthenewguessandsteps2through6 repeated. Asafurthercheck,thevalueofRavecanberecalculatedandEq.(10.56)solvedforΔNp.Again,if thenewvalueagreeswithwhatwaspreviouslycalculatedinstep3withinsometolerance,itcan beassumedthattheoilrecoveryiscorrect.ThethreemethodsareillustratedinExample10.1. Table 10.4 Fluid Property Data for Example 10.1 Pressure (psia) Bo (bbl/STB) Rso (SCF/STB) Bg (bbl/SCF) μo (cp) μg (cp) 2500 1.498 721 0.001048 0.488 0.0170 2300 1.463 669 0.001155 0.539 0.0166 2100 1.429 617 0.001280 0.595 0.0162 1900 1.395 565 0.001440 0.658 0.0158 1700 1.361 513 0.001634 0.726 0.0154 1500 1.327 461 0.001884 0.802 0.0150 1300 1.292 409 0.002206 0.887 0.0146 1100 1.258 357 0.002654 0.981 0.0142 900 1.224 305 0.003300 1.085 0.0138 700 1.190 253 0.004315 1.199 0.0134 500 1.156 201 0.006163 1.324 0.0130 300 1.121 149 0.010469 1.464 0.0126 100 1.087 97 0.032032 1.617 0.0122 10.3 Immiscible Displacement Processes 393 Example 10.1 Calculating Oil Recovery as a Function of Pressure Thisexampleusesthe(1)Muskat,(2)Schilthuis,and(3)Tarnermethodsforanundersaturated, volumetricreservoir.Therecoveryiscalculatedforthefirst200-psipressureincrementfromthe initialpressuredowntoapressureof2300psia. Given Initialreservoirpressure=2500psia Initialreservoirtemperature=180°F Initialoilinplace=56×106 STB Initialwatersaturation=0.20 FluidpropertydataaregiveninTable10.4. PermeabilityratiodataareplottedinFig.10.16. Solution TheMuskatmethodinvolvesthefollowingsequenceofsteps: 1.Rso, Bo,and1/Bgareplottedversuspressuretodeterminetheslopes.Althoughtheplots arenotshown,thefollowingvaluescanbedetermined: dRso = 0.26 dp dBo = 0.000171 dp d (1 / Bg ) dp = 0.433 ThevaluesofX(p),Y(p),andZ(p)aretabulatedasfollows,asafunctionofpressure: Pressure X(p) Y(p) Z(p) 2500psia 0.000182 0.003277 0.000454 2300psia 0.000205 0.003795 0.000500 2.CalculateΔSo/ΔpusingX(p),Y(p),andZ(p)at2500psia: kg So X ( p ) + So Y ( p ) − (1 − So − Sw )Z ( p ) ko ΔSo = Δp kg μo 1+ ko μ g ΔSo 0.20(0.000182 ) + 0 + 0 = = 0.000146 Δp 1+ 0 (10.36) Chapter 10 394 • The Displacement of Oil and Gas 3.EstimateSoj: ΔS Soj = So( j −1) − Δp o Δp (10.38) Soj=0.80–200(0.000146)=0.7709 4.CalculateΔSo/ΔpusingtheSojfromstep3andX(p),Y(p),andZ(p)at2300psia: kg So X ( p ) + So Y ( p ) − (1 − So − Sw )Z ( p ) ko ΔSo = Δp kg μo 1+ k μ o g (10.36) 0.7709(0.000205 ) + 0.7709(0.00001)0.003795 ΔSo = Δp + (1.0 − 0.2 − 0.7709 )0.000500 0.539 1+ (00.00001) 0.0166 ΔSo = 0.000173 Δp 5.CalculatetheaverageΔSo/Δp: 0.000146 + 0.000173 ΔSo = 0.000159 Δp = 2 ave 6.CalculateSojusing(ΔSoΔp)avefromstep5: ΔS Soj = So( j −1) − Δp o Δp (10.38) Soj=0.8–0.000159(200)=0.7682 ThisvalueofSocannowbeusedtocalculatetheoilrecoverythathasoccurreddown toapressureof2300psia: 10.3 Immiscible Displacement Processes 395 S B N p = N 1.0 − o oi 1 − Sw Bo (10.57) 0.7682 1.498 N p = 56(10 )6 1.0 − = 939, 500 STB 1 − 0.2 1.463 BecausetheSchilthuismethodinvolvesaninteractiveprocedure,aniterativesolver,like Excel’ssolver,isusedtoassistinthesolution.Forthisproblem,Np/Nistheguessvaluethatthe solverwillusetosolveEq.(10.41).ThesolverrequiresoneguessvalueofNp/Ntobeginthe iterationprocess. 1.Assumeincrementaloilrecovery: ΔN p1 N = 0.01 2.CalculateSL: N p Bo SL = Sw + (1 − Sw ) 1 − N Boi (10.40) 3.Determinekg/kofromFig.10.16andcalculateR: kg ko1 kg = ko 2 = 0.00001 R = Rso + kg μo Bo ko μg Bg (10.33) R1=721 0.539 1.463 = 669.4 R2 = 669 + 0.00001 0.0166 0.001155 4.Calculateincrementalgasrecovery: Rave = R j −1 + R j 2 (10.43) Chapter 10 396 • The Displacement of Oil and Gas kg/ko 10 kg/ko 5 2 1 100 0.5 50 0.2 20 0.1 10 0.05 5 0.02 2 0.01 1 0.005 0.5 0.002 0.2 0.001 30 40 50 60 70 80 90 100 0.1 Total liquid saturation, % Figure 10.16 Permeability ratio relationship for Example 10.1. Rave = 721 + 669.4 = 695.2 2 ΔG p N ΔG p1 N = ΔN p N ( Rave ) (10.44) = 0.01(695.2 ) = 6.952 5.CalculateRp: Rp = Rp = Gp / N Np / N 6.952 = 695.2 0.01 (10.46) 10.3 Immiscible Displacement Processes 397 6.UseExcel’ssolverfunctiontosolveEq.(10.41)iterativelybychangingNp/Nuntilthe left-handsideofEq.(10.41)isequaltozero: Np [ Bo + Bg ( Rp − Rso )] N −1 = 0 Bo − Boi + Bg ( Rsoi − Rso ) (10.41) Usingthismethod,thecorrectvalueoffractionaloilrecoverydownto2300psiais 0.0165.TocomparewiththeMuskatmethod,therecoveryratiomustbemultipliedbythe initialoilinplace,56MSTB,toyieldthetotalcumulativerecovery: Np=56(10)6(0.0167)=935,200STB TheTarnermethodrequiresthefollowingsteps: 1.CalculateΦn and Φgat2300psia: Φn = Bo − Boi + ( Rsoi Bo − Rso Bg mBoi − Rso ) Bg + + ( Bg − Bgi ) Bgi (10.49) Chapter 10 398 Φn = The Displacement of Oil and Gas 1.463 − 669(0.001155 ) = 27.546 1.463 − 1.498 + ( 721 − 669 )0.001155 Φg = Φg = • Bg Bo − Boi + ( Rsoi − Rso ) Bg + mBoi + ( Bg − Bgi ) Bgi (10.50) 0.001155 = 0.04609 1.463 − 1.498 + ( 721 − 669 )0.001155 2.AssumeRj=670SCF/STB,whichisjustslightlylargerthanRso,suggestingthatonlya verysmallamountofgasisflowingtothewellboreandisbeingproduced: Rave = 721 + 670 = 695.5 2 3.CalculateΔNp: ΔN p = ΔN p = N − N p( j −1) Φ n − G p( j −1) Φ g Φ n + Φ g Rave (10.56) 56, 000, 000 − 0 − 0 = 939, 300 STB 27.546 + 0.04609(695.9 ) 4.CalculateNp: Npj = Np(j–1) + ΔNp (10.55) Np = ΔNp =939,300STB 5.Determinekg/ko: N p Bo SL = Sw + (1 − Sw ) 1 − N Boi 939, 300 1.463 SL = 0.2 + (1 − 0.2 ) 1 − = 0.968 56 , 000, 000 1.498 (10.40) Problems 399 FromthisvalueofSL,thepermeabilityratio,kg/ko,canbeobtainedfromFig.10.16. Sincethecurveisofftheplot,averysmallvalueofkg/ko=0.00001isestimated. 6.CalculateRjandcompareitwiththeassumedvalueinstep2: R = Rso + kg μo Bo ko μg Bg (10.33) 0.539 1.463 = 669.4 R j = 669 + 0.00001 0.0166 0.001155 Thisvalueagreesverywellwiththevalueof670thatwasassumedinstep2,satisfying theconstraintsoftheTarnermethod.Forthedatagiveninthisexample,thethreemethods ofcalculationyieldedvaluesofNpthatarewithin0.5%.Thissuggeststhatanyoneofthe three methods may be used to predict oil and gas recovery, especially considering that manyoftheparametersusedintheequationscouldbeinerrormorethan0.5%. 10.4 Summary Theintentofthischapterwastopresentfundamentalconceptsthatcanhelpreservoirengineers understandtheimmiscibledisplacementofoilandgas.Manypracticingengineerswillneedto addthetoolofreservoirsimulationtotheconceptsdiscussedinthischapter.Thesimulationof reservoirsinvolvesmanyoftheequationsthathavebeenpresentedinthischapter,alongwithmuch moreinvolvedmathematicsandcomputerprogramming.Theinterestedreaderisreferredtoanumberofpublishedworksthatdescribetheimportantfieldofreservoirsimulation.19–22 Problems 10.1 (a) A rock10cmlongand2cm2incrosssectionflows0.0080cm3/secofa2.5-cpoilundera 1.5-atmpressuredrop.Iftheoilsaturatestherock100%,whatisitsabsolutepermeability? (b) Whatwillbetherateof0.75-cpbrineinthesamecoreundera2.5-atmpressuredrop ifthebrinesaturatestherock100%? (c) Istherockmorepermeabletotheoilat100%oilsaturationortothebrineat100% brinesaturation? (d) Thesamecoreismaintainedat40%watersaturationand60%oilsaturation.Undera 2.0-atmpressuredrop,theoilflowis0.0030cm3/secandthewaterflowis0.004cm3/ sec.Whataretheeffectivepermeabilitiestowaterandtooilatthesesaturations? (e) Explain why the sum of the two effective permeabilities is less than the absolute permeability. Chapter 10 400 • The Displacement of Oil and Gas (f) Whataretherelativepermeabilitiestooilandwaterat40%watersaturation? (g) Whatistherelativepermeabilityratioko/kwat40%watersaturation? (h) Showthattheeffectivepermeabilityratioisequaltotherelativepermeabilityratio. 10.2 Thefollowingpermeabilitydataweremeasuredonasandstoneasafunctionofitswater saturation: a Sw 0 10 20 30a 40 50 60 70 75 80 90 100 kro 1.0 1.0 1.0 0.94 0.80 0.44 0.16 0.045 0 0 0 0 krw 0 0 0 0 0.04 0.11 0.20 0.30 0.36 0.44 0.68 1.0 Criticalsaturationsforoilandwater (a) PlottherelativepermeabilitiestooilandwaterversuswatersaturationonCartesian coordinatepaper. (b) Plottherelativepermeabilityratioversuswatersaturationonsemilogpaper. (c) Findtheconstantsa and binEq.(10.3)fromtheslopeandinterceptofyourgraph. Alsofinda and bbysubstitutingtwosetsofdatainEq.(10.3)andsolvingsimultaneousequations. (d) If μo=3.4cp, μw=0.68cp,Bo=1.50bbl/STB,andBw=1.05bbl/STB,whatisthe surfacewatercutofawellcompletedinthetransitionzonewherethewatersaturation is50%? (e) Whatisthereservoirwatercutinpart(d)? (f) Whatpercentageofrecoverywillberealizedfromthissandstoneunderhigh-pressure waterdrivefromthatportionofthereservoirabovethetransitionzoneinvadedbywater?Theinitialwatersaturationabovethetransitionzoneis30%. (g) Ifwaterdriveoccursatapressurebelowsaturationpressuresuchthattheaveragegas saturationis15%intheinvadedportion,whatpercentageofrecoverywillberealized? Theaverageoilvolumefactoratthelowerpressureis1.35bbl/STBandtheinitialoil volumefactoris1.50bbl/STB. (h) Whatfractionoftheabsolutepermeabilityofthissandstoneisduetotheleastpermeableporechannelsthatmakeup20%oftheporevolume?Whatfractionisduetothe mostpermeableporechannelsthatmakeup25%oftheporevolume? 10.3 Giventhefollowingreservoirdata, Throughputrate=1000bbl/day Averageporosity=18% Initialwatersaturation=20% Cross-sectionalarea=50,000ft2 Waterviscosity=0.62cp Problems 401 Oilviscosity=2.48cp ko/kwversusSwdatainFigs.10.1and10.2 assumezerotransitionzoneand (a) CalculatefwandplotversusSw. (b) Graphicallydetermine∂fw/∂SwatanumberofpointsandplotversusSw. (c) Calculate∂fw/∂SwatseveralvaluesofSwusingEq.(10.17),andcomparewiththegraphicalvaluesofpart(b). (d) Calculatethedistancesofadvanceoftheconstantsaturationfrontsat100,200,and 400days.PlotonCartesiancoordinatepaperversusSw.Equalizetheareaswithinand withoutthefloodfrontlinestolocatethepositionofthefloodfronts. (e) DrawasecantlinefromSw=0.20tangenttothefwversusSwcurveinpart(b),andshow thatthevalueofSwatthepointoftangencyisalsothepointatwhichthefloodfront lines are drawn. (f) Calculatethefractionalrecoverywhenthefloodfrontfirstinterceptsawell,usingthe areasofthegraphofpart(d).Expresstherecoveryintermsofboththeinitialoilin placeandtherecoverableoilinplace(i.e.,recoverableafterinfinitethroughput). (g) Towhatsurfacewatercutwillawellrathersuddenlyrisewhenitisjustenvelopedby thefloodfronts?UseBo=1.50bbl/STBandBw=1.05bbl/STB. (h) Dotheanswerstoparts(f)and(g)dependonhowfarthefronthastraveled?Explain. 10.4 Showthatforradialdisplacementwhererw <<, 5.615 qt′ ∂fw r= πϕ h ∂Sw 1/2 whereristhedistanceaconstantsaturationfronthastraveled. 10.5 Giventhefollowingreservoirdata, Sg kg/ko kro a 10a 15 20 25 30 35 40 45 50 0 0.08 0.20 0.40 0.85 1.60 3.00 5.50 10.0 0.70 0.52 0.38 0.28 0.20 0.14 0.11 0.07 0.04 Criticalsaturationsforgasandoil Absolutepermeability=400md Hydrocarbonporosity=15% Connatewater=28% Dipangle=20° 62a 0 Chapter 10 402 • The Displacement of Oil and Gas Cross-sectionalarea=750,000ft2 Oilviscosity=1.42cp Gasviscosity=0.015cp Reservoiroilspecificgravity=0.75 Reservoirgasspecificgravity=0.15(water=1) Reservoirthroughputatconstantpressure=10,000bbl/day (a) Calculateandplotthefractionofgas,fg,versusgassaturationsimilartoFig.10.13both withandwithoutthegravitysegregationterm. (b) Plotthegassaturationversusdistanceafter100daysofgasinjectionbothwithand withoutthegravitysegregationterm. (c) Usingtheareasofpart(b),calculatetherecoveriesbehindthefloodfrontwithand withoutgravitysegregationintermsofbothinitialoilandrecoverableoil. 10.6 Deriveanequation,includingagravitytermsimilartoEq.(10.23)forwaterdisplacingoil. 10.7 ReworkthewaterdisplacementcalculationofTable10.1,andincludeagravitysegregation term.Assumeanabsolutepermeabilityof500md,adipangleof45°,andadensitydifferenceof20%betweenthereservoiroilandwaterandanoilviscosityof1.6cp.Plotwater saturationversusdistanceafter240daysandcomparewithFig.10.11. Sw 20 30 40 50 60 70 80 90 kro 0.93 0.60 0.35 0.22 0.12 0.05 0.01 0 10.8 ContinuethecalculationsofProblem10.1downtoareservoirpressureof100psia,using (a) Muskatmethod (b) Schilthuismethod (c) Tarnermethod References 1. G.PWillhite,Waterflooding,Vol.3,SocietyofPetroleumEngineers,1986. 2. F. F. Craig, The Reservoir Engineering Aspects of Waterflooding, Society of Petroleum Engineers,1993. 3. L.W.Lake,Enhanced Oil Recovery,PrenticeHall,1989. 4. D.W.GreenandG.P.Willhite,Enhanced Oil Recovery,Vol.6,SocietyofPetroleumEngineers,1998. References 403 5. E.D.Holstein,ed.,Petroleum Engineering Handbook,Vol.5, Reservoir Engineering and Petrophysics,SocietyofPetroleumEngineers,2007. 6. R. D. Wycoff, H. G. Botset, and M. Muskat, “Mechanics of Porous Flow Applied to Water-FloodingProblems,”Trans.AlME(1933),103,219. 7. R.L.SlobodandB.H.Candle,“X-rayShadowgraphStudiesofArealSweepEfficiencies,” Trans.AlME(1952),195,265. 8. S.E.BuckleyandM.C.Leverett,“MechanismofFluidDisplacementinSands,”Trans.AlME (1942),146,107. 9. J.G.RichardsonandR.J.Blackwell,“UseofSimpleMathematicalModelsforPredicting ReservoirBehavior,”Jour. of Petroleum Technology(Sept.1971),1145. 10. H.J.Welge,“ASimplifiedMethodforComputingOilRecoveriesbyGasorWaterDrive,” Trans.AlME(1952),195,91. 11. D. R. Shreve and L.W.Welch Jr., “Gas Drive and Gravity DrainageAnalysis for Pressure MaintenanceOperations,”Trans.AlME(1956),207,136. 12. L.R.Kern,“DisplacementMechanisminMulti-wellSystems,”Trans.AlME(1952),195,39. 13. R.H.SmithreportedbyJ.A.Klotz,“TheGravityDrainageMechanism,”Jour. of Petroleum Technology(Apr.1953),5,19. 14. M. Muskat, “The Production Histories of Oil Producing Gas-Drive Reservoirs,” Jour. of Applied Physics(1945),16,147. 15. E.T.Guerrero,Practical Reservoir Engineering,PetroleumPublishingCo.,1968. 16. J.Tarner,“HowDifferentSizeGasCapsandPressureMaintenanceProgramsAffectAmount ofRecoverableOil,”Oil Weekly(June12,1944),144,32–34. 17. J. B. Riggs, An Introduction to Numerical Methods for Chemical Engineers,TexasTech. UniversityPress,1988. 18. G.W.Tracy,“SimplifiedFormoftheMaterialBalanceEquation,”Trans.AlME(1955),204, 243. 19. T.Ertekin,J.H.Abou-Kassem,andG.R.King,Basic Applied Reservoir Simulation,Vol.10, SocietyofPetroleumEngineers,2001. 20. J.Fanchi,Principles of Applied Reservoir Simulation,3rded.,Elsevier,2006. 21. C.C.MattaxandR.L.Dalton,Reservoir Simulation,Vol.13,SocietyofPetroleumEngineers, 1990. 22. M.Carlson,Practical Reservoir Simulation,PennWellPublishing,2006. This page intentionally left blank C H A P T E R 1 1 Enhanced Oil Recovery 11.1 Introduction Theinitialproductionofhydrocarbonsfromanoil-bearingformationisaccomplishedbytheuse ofnaturalreservoirenergy.AsdiscussedinChapter1,thistypeofproductionistermedprimary production. Sources of natural reservoir energy that lead to primary production include the swellingofreservoirfluids,thereleaseofsolutiongasasthereservoirpressuredeclines,nearby communicatingaquifers,andgravitydrainage.Whenthenaturalreservoirenergyhasbeendepleted,itbecomesnecessarytoaugmentthenaturalenergyfromanexternalsource.TheSocietyof PetroleumEngineershasdefinedthetermenhanced oil recovery (EOR)asthefollowing:“oneor moreofavarietyofprocessesthatseektoimproverecoveryofhydrocarbonfromareservoirafter theprimaryproductionphase.”1 TheseEORtechniqueshavebeenlumpedintotwocategories—secondaryandtertiaryrecoveryprocesses.Itistheseprocessesthatprovidetheadditionalenergytoproduceoilfromreservoirs inwhichtheprimaryenergyhasbeendepleted. Typically, the first attempt to supply energy from an external source is accomplished by theinjectionofanimmisciblefluid—eitherwater,referredtoaswaterflooding,oranaturalgas, referredtoasgasflooding.Theuseofthisinjectionschemeiscalledasecondaryrecoveryoperation.Frequently,themainpurposeofeitherawateroragasinjectionprocessistorepressurizethe reservoirandthenmaintainthereservoiratahighpressure.Hencethetermpressure maintenance issometimesusedtodescribemostsecondaryrecoveryprocesses. Tertiary recovery processes were developed for application in situations where secondary processeshadbecomeineffective.However,thesametertiaryprocesseswerealsoconsideredfor reservoirapplicationswheresecondaryrecoverytechniqueswerenotusedbecauseoflowrecovery potential.Inthelattercase,thenametertiaryisamisnomer.Formostreservoirs,itisadvantageous tobeginasecondaryoratertiaryprocessconcurrentwithprimaryproduction.Fortheseapplications,thetermEORwasintroduced. Aprocessthatisnotdiscussedinthistextistheuseofpumpjacksattheendofprimary production.Apumpjackisbasicallyadeviceusedwithadownholepumptohelpliftoilfromthe 405 Chapter 11 406 • Enhanced Oil Recovery reservoirwhenthereservoirpressurehasbeendepletedtoapointwheretheoilcannottravelto thesurface.Mostproducingcompanieswillemploythistechnology,butitisnotconsideredan enhancedoilrecoveryprocess. On the average, primary production methods will produce from a reservoir about 25% to 30%oftheinitialoilinplace.Theremainingoil,70%to75%oftheinitialresource,isalargeand attractivetargetforenhancedoilrecoverytechniques.Thischapterwillprovideanintroductionto themaintypesofEORtechniquesthathavebeenusedintheindustry.Muchoftheinformation inthischapterhasbeentakenfromanarticlewrittenbyoneoftheauthorsandpublishedinthe Encyclopedia of Physical Science and Technology(thirdedition).2Theinformationisusedwith permissionfromElsevier. 11.2 Secondary Oil Recovery As mentioned in the previous section, there are in general two types of secondary recovery processes—waterfloodingandgasflooding.Thesewillbothbediscussedinthissection.Waterfloodinghasbeenthemostusedprocess,butgasfloodinghasprovenveryusefulwithreservoirs withagascapandwherethehydrocarbonformationhasasignificantdipstructuretoit. Waterfloodingrecoversoilbythewatermovingthroughthereservoirasabankoffluidand “pushing”oilaheadofit.Therecoveryefficiencyofawaterfloodislargelyafunctionofthesweep efficiencyofthefloodandtheratiooftheoilandwaterviscosities.Sweepefficiency,asdiscussed inChapter10,isameasureofhowwellthewaterhascontactedtheavailableporespaceinthe oil-bearingzone.Grossheterogeneitiesintherockmatrixleadtolowsweepefficiencies.Fractures, high-permeability streaks, and faults are examples of gross heterogeneities. Homogeneous rock formationsprovidetheoptimumsettingforhighsweepefficiencies.Wheninjectedwaterismuch lessviscousthantheoilitismeanttodisplace,thewatercouldbegintofingerorchannelthrough thereservoir.AsdiscussedinChapter10,section2.3,thisfingeringorchannelingisreferredto as viscous fingeringandmayleadtosignificantbypassingofresidualoilandlowerfloodingefficiencies.Thisbypassingofresidualoilisanimportantissueinapplyinganyenhancedoilrecovery technique,includingwaterflooding. Gasisalsousedinasecondaryrecoveryprocesscalledgasflooding.Whengasisthepressuremaintenanceagent,itisusuallyinjectedintoazoneoffreegas(i.e.,agascap)tomaximize recoverybygravitydrainage.Theinjectedgasisusuallyproducednaturalgasfromthereservoirin question.This,ofcourse,defersthesaleofthatgasuntilthesecondaryoperationiscompletedand thegascanberecoveredbydepletion.Othergases,suchasN2 and CO2,canbeinjectedtomaintain reservoirpressure.Thisallowsthenaturalgastobesoldasitisproduced. 11.2.1 Waterflooding Thewaterfloodingprocesswasdiscoveredquitebyaccidentmorethan100yearsagowhenwater fromashallowwater-bearinghorizonleakedaroundapackerandenteredanoilcolumninawell. Theoilproductionfromthewellwascurtailed,butproductionfromsurroundingwellsincreased. Overtheyears,theuseofwaterfloodinggrewslowlyuntilitbecamethedominantfluidinjection 11.2 Secondary Oil Recovery 407 recoverytechnique.Inthefollowingsections,anoverviewoftheprocessisprovided,including information regarding the characteristics of good waterflood candidates and the location of injectorsandproducersinawaterflood.Waystoestimatetherecoveryofawaterfloodarebriefly discussed.Thereaderisreferredtoseveralgoodreferencesonthesubjectthatprovidedetailed designcriteria.3–7 11.2.1.1 Waterflooding Candidates Severalfactorslendanoilreservoirtoasuccessfulwaterflood.Theycanbegeneralizedintwo categories:reservoircharacteristicsandfluidcharacteristics. Themainreservoircharacteristicsthataffectawaterfloodaredepth,structure,homogeneity, andpetrophysicalpropertiessuchasporosity,saturation,andaveragepermeability.Thedepthof thereservoiraffectsthewaterfloodintwoways.First,investmentandoperatingcostsgenerally increaseasthedepthincreases,asaresultoftheincreaseindrillingandliftingcosts.Second,the reservoirmustbedeepenoughfortheinjectionpressuretobelessthanthefracturepressureofthe reservoir.Otherwise,fracturesinducedbyhighwaterinjectionratescouldleadtopoorsweepefficienciesiftheinjectedwaterchannelsthroughthereservoirtotheproducingwells.Ifthereservoir hasadippedstructure,gravityeffectscanoftenbeusedtoincreasesweepefficiencies.Thehomogeneityofareservoirplaysanimportantroleintheeffectivenessofawaterflood.Thepresence offaults,permeabilitytrends,andthelikeaffectthelocationofnewinjectionwellsbecausegood communicationisrequiredbetweeninjectionandproductionwells.However,ifseriouschanneling exists,asinsomereservoirsthataresignificantlyheterogeneous,thenmuchofthereservoiroilwill bebypassedandthewaterinjectionwillberendereduseless.Ifareservoirhasinsufficientporosity andoilsaturation,thenawaterfloodmaynotbeeconomicallyjustified,onthebasisthatnotenough oilwillbeproducedtooffsetinvestmentandoperatingcosts.Theaveragereservoirpermeability shouldbehighenoughtoallowsufficientfluidinjectionwithoutpartingorfracturingthereservoir. Theprincipalfluidcharacteristicistheviscosityoftheoilcomparedtothatoftheinjected water.Theimportantvariabletoconsiderisactuallythemobilityratio,whichwasdefinedearlier inChapter8andincludesnotonlytheviscosityratiobutalsoaratiooftherelativepermeabilities toeachfluidphase: M = kw / μ w ko / μ o Agoodwaterfloodhasamobilityratioaround1.Ifthereservoiroilisextremelyviscous,thenthe mobilityratiowilllikelybemuchgreaterthan1,viscousfingeringwilloccur,andthewatermay bypassmuchoftheoil. 11.2.1.2 Location of Injectors and Producers Theinjectionandproductionwellsinawaterfloodshouldbeplacedtoaccomplishthefollowing: (1)providethedesiredoilproductivityandthenecessarywaterinjectionratetoyieldthisoilproductivityand(2)takeadvantageofthereservoircharacteristics,suchasdip,faults,fractures,and Chapter 11 408 • Enhanced Oil Recovery permeabilitytrends.Ingeneral,twokindsoffloodingpatternsareused:peripheralfloodingand patternflooding. Patternfloodingisusedinreservoirshavingasmalldipandalargesurfacearea.Someof themorecommonpatternsareshowninFig.11.1.Table11.1liststheratioofproducingwells toinjectionwellsinthepatternsshowninFig.11.1.Ifthereservoircharacteristicsyieldlower injectionratesthanthosedesired,theoperatorshouldconsiderusingeitheraseven-oraninespotpattern,wheretherearemoreinjectionwellsperpatternthanproducingwells.Asimilar argument can be made for using a four-spot pattern in a reservoir with low flow rates in the productionwells. Four spot Five spot Seven spot Nine spot Direct-line drive Staggered-line drive Producing well Injection well Figure 11.1 Geometry of common pattern floods. 11.2 Secondary Oil Recovery Table 11.1 409 Ratio of Producing Wells to Injection Wells for Several Pattern Arrangements Pattern Ratio of producing wells to injection wells Fourspot 2 Fivespot 1 Sevenspot 1/2 Ninespot 1/3 Direct-linedrive 1 Staggered-linedrive 1 Thedirect-linedriveandstaggered-linedrivepatternsarefrequentlyusedbecausetheyusuallyinvolvethelowestinvestment.Someoftheeconomicfactorstoconsiderincludethecostof drillingnewwells,thecostofswitchingexistingwellstoadifferenttype(i.e.,aproducertoan injector),andthelossofrevenuefromtheproductionwhenmakingaswitchfromaproducerto aninjector. Inperipheralflooding,theinjectorsaregroupedtogether,unlikeinpatternfloodswherethe injectorsareinterspersedwiththeproducers.Figure11.2illustratestwocasesinwhichperipheral floodsaresometimesused.InFig.11.2(a),aschematicofananticlinalreservoirwithanunderlying aquiferisshown.Theinjectorsareplacedsothattheinjectedwatereitherenterstheaquiferoris neartheaquifer-reservoirinterface.Thepatternofwellsonthesurface,showninFig.11.2(a),isa ringofinjectorssurroundingtheproducers.Amonoclinalreservoirwithanunderlyingaquiferis showninFig.11.2(b).Inthiscase,theinjectorsareagainplacedsothattheinjectedwatereither enterstheaquiferorentersneartheaquifer-reservoirinterface.Whenthisisdone,thewellarrangementshowninFig.11.2(b),wherealltheinjectorsaregroupedtogether,isobtained. Sincethe1990s,otherwaterinjectionsschemeshavebeenused.Theseincludehorizontal wells and injection pressures above the reservoir fracturing pressure.The use of these schemes hasresultedinmixedsuccess.Thereaderisencouragedtopursuetheliteraturetoresearchthese techniquesiffurtherinterestiswarranted.6–9 11.2.1.3 Estimation of Waterflood Recovery Efficiency Equation (11.1) is an expression for the overall recovery efficiency for any fluid displacement process: E = EvEd where E=overallrecoveryefficiency Ev=volumetricdisplacementefficiency Ed=microscopicdisplacementefficiency (11.1) Chapter 11 410 • Enhanced Oil Recovery Oil Water (a) Oil Water (b) Figure 11.2 Well arrangements for (a) anticlinal and (b) monoclinal reservoirs with underlying aquifers. Thevolumetricdisplacementefficiencyismadeupofthearealdisplacementefficiency,Es,andthe verticaldisplacementefficiency,Ei.Toestimatetheoverallrecoveryefficiency,valuesforEs, Ei, and Edmustbeestimated.Methodsofestimatingthesetermsarediscussedinwaterfloodtextbooks andaretoolengthytopresentindetailhere.3–7However,somebrief,generalcommentsconcerning eachofthedisplacementefficienciescanbemade. Thereareseveralmethodsofobtainingestimatesforthemicroscopicdisplacementefficiency.Thebasisforonemethodwaspresentedinsection10.3.1inChapter10.Thearealdisplacement, or sweep, efficiency is largely a function of pattern type and mobility ratio.The vertical displacementefficiencyisprimarilyafunctionofreservoirheterogeneitiesandthicknessofthe reservoirformation. Waterfloodingisanimportantprocessforthereservoirengineertounderstand.Asuccessfulwaterfloodinatypicalreservoirresultsinoilrecoveriesincreasingfrom25%afterprimary 11.2 Secondary Oil Recovery 411 recoveryto30%to33%overall.Ithasmadeandwillcontinuetomakelargecontributionstothe recoveryofreservoiroil. 11.2.2 Gasflooding GasfloodingwasintroducedinChapter5,sections5.6and5.7,wheretheinjectionofanimmisciblegaswasdiscussedinretrogradegasreservoirs.Gasisfrequentlyinjectedinthesetypesof reservoirstomaintainthepressureatalevelabovethepointatwhichliquidwillbegintocondense inthereservoir.10,11Thisisdonebecauseofthevalueoftheliquidandthepotentialtoproducethe liquidonthesurface.Reservoirgasisalsopushedtotheproducingwellsbytheinjectedgas,similartooilbeingpushedbyawaterflood,asdiscussedintheprevioussection. AsecondtypeofgasfloodingisthatshowninFig.11.3.Adrygasisinjectedintothegas capofasaturatedoilreservoir.Thisisdonetomaintainreservoirpressureandalsoforthegas captopushdownontheoil-bearingformation.Thusoilispushedtotheproducingwells.Obviously,theproducingwellsshouldbeperforatedintheliquidzonesothattheproductionofoil willbemaximized. Steeply dipping reservoirs may yield high sweep efficiencies and high oil recoveries.A concerningasfloodinginmorehorizontalstructuresistheviscosityratioofthegastooil.Since agasistypicallymuchlessviscousthanoil,viscousfingeringofthegasphasethroughtheoil phasemayoccur,resultinginpoorsweepefficienciesandlowoilrecoveries.Ofteninhorizontalreservoirs,tohelpwiththepoorsweepefficiencies,waterisinjectedafteranamountofgas injection.Thewaterisfollowedbymoregas.Thisprocessisreferredtoasthewater alternating gasinjectionprocess,orWAG.Christensenetal.haveshowntheeffectivenessofthisprocessin severalapplications.12 CO2 CO2 Oil Figure 11.3 Schematic of a typical gasflooding project in an undersaturated oil reservoir. Chapter 11 412 • Enhanced Oil Recovery As discussed in Chapter 5, N2 and CO2 have been used in gasflooding projects.With the increased desire to sequester CO2, the injection of CO2 has developed into a viable option as a secondaryrecoveryprocess.13–15 11.3 Tertiary Oil Recovery Tertiaryoilrecoveryreferstotheprocessofproducingliquidhydrocarbonsbymethodsotherthanthe conventionaluseofreservoirenergy(primaryrecovery)andsecondaryrecoveryschemesdiscussed inthelastsection.Inthistext,tertiaryoilrecoveryprocesseswillbeclassifiedintothreecategories: (1)misciblefloodingprocesses,(2)chemicalfloodingprocesses,and(3)thermalfloodingprocesses. The category of miscible displacement includes single-contact and multiple-contact miscible processes.Chemicalprocessesarepolymer,micellarpolymer,alkalineflooding,andmicrobialflooding. Thermalprocessesincludehotwater,steamcycling,steamdrive,andinsitucombustion.Ingeneral, thermal processes are applicable in reservoirs containing heavy crude oils, whereas chemical and miscibledisplacementprocessesareusedinreservoirscontaininglightcrudeoils.Thenextfewsectionsprovideanintroductiontotheseprocesses.Ifinterested,thereaderisagainreferredtoseveral goodreferencesonthesubjectthatprovidedetaileddesigncriteria.6,7,16–20 11.3.1 Mobilization of Residual Oil Duringtheearlystagesofawaterfloodinawater-wetreservoirsystem,thebrineexistsasafilm aroundthesandgrains,andtheoilfillstheremainingporespace.Atanintermediatetimeduring theflood,theoilsaturationhasbeendecreasedandexistspartlyasacontinuousphaseinsome porechannelsbutasdiscontinuousdropletsinotherchannels.Attheendoftheflood,whentheoil hasbeenreducedtoresidualoilsaturation,Sor,theoilexistsprimarilyasadiscontinuousphaseof dropletsorglobulesthathavebeenisolatedandtrappedbythedisplacingbrine. Thewaterfloodingofoilinanoil-wetsystemyieldsadifferentfluiddistributionatSor. Early inthewaterflood,thebrineformscontinuousflowpathsthroughthecenterportionsofsomeofthe porechannels.Thebrineentersmoreandmoreoftheporechannelsasthewaterfloodprogresses. Atresidualoilsaturation,thebrinehasenteredasufficientnumberofporechannelstoshutoffthe oilflow.Theresidualoilexistsasafilmaroundthesandgrains.Inthesmallerflowchannels,this filmmayoccupytheentirevoidspace. Themobilizationoftheresidualoilsaturationinawater-wetsystemrequiresthatthediscontinuousglobulesbeconnectedtoformacontinuousflowchannelthatleadstoaproducingwell.In anoil-wetporousmedium,thefilmofoilaroundthesandgrainsmustbedisplacedtolargepore channelsandbeconnectedinacontinuousphasebeforeitcanbemobilized.Themobilizationof oilisgovernedbytheviscousforces(pressuregradients)andtheinterfacialtensionforcesthat existinthesandgrain–oil–watersystem. Therehavebeenseveralinvestigationsoftheeffectofviscousforcesandinterfacialtension forces on the trapping and mobilization of residual oil.4–7,17,21,22 From these studies, correlations betweenadimensionlessparametercalledthecapillary number, Nvc,andfractionofoilrecovered 11.3 Tertiary Oil Recovery 413 havebeendeveloped.Thecapillarynumberistheratiooftheviscousforcetotheinterfacialtension forceandisdefinedbyEq.(11.2). N vc = (constant) υμw k Δp = (constant) o σ ow ϕσ ow L (11.2) whereυisvelocity,μwistheviscosityofthedisplacingfluid,σowistheinterfacialtensionbetween thedisplacedanddisplacingfluids,koistheeffectivepermeabilitytothedisplacedphase,φisthe porosity,andΔp/Listhepressuredropassociatedwiththevelocity. Figure11.4isaschematicrepresentationofthecapillarynumbercorrelationinwhichthe capillary number is plotted on the abscissa, and the ratio of residual oil saturation (value after conductingatertiaryrecoveryprocesstothevaluebeforethetertiaryrecoveryprocess)isplotted astheverticalcoordinate.Thecapillarynumberincreasesastheviscousforceincreasesorasthe interfacialtensionforcedecreases. Thecorrelationsuggeststhatacapillarynumbergreaterthan10–5forthemobilizationofunconnectedoildropletsisnecessary.Thecapillarynumberincreasesastheviscousforceincreases orastheinterfacialtensionforcedecreases.Thetertiarymethodsthathavebeendevelopedand appliedtoreservoirsituationsaredesignedeithertoincreasetheviscousforceassociatedwiththe 1 (SOR ) after (SOR ) before 0.5 0 10–8 10–7 10–6 10–5 10–4 Capillary number Figure 11.4 Capillary number correlation. 10–3 10–2 Chapter 11 414 • Enhanced Oil Recovery injectedfluidortodecreasetheinterfacialtensionforcebetweentheinjectedfluidandthereservoir oil.Thenextsectionsdiscussthefourgeneraltypesoftertiaryprocesses:miscibleflooding,chemicalflooding,thermalflooding,andmicrobialflooding. 11.3.2 Miscible Flooding Processes InChapter10,itwasnotedthatthemicroscopicdisplacementefficiencyislargelyafunctionofinterfacialforcesactingbetweentheoil,rock,anddisplacingfluid.Iftheinterfacialtensionbetween thetrappedoilanddisplacingfluidcouldbeloweredto10–2to10–3dynes/cm,theoildropletscould bedeformedandsqueezethroughtheporeconstrictions.Amiscibleprocessisoneinwhichthe interfacialtensioniszero—thatis,thedisplacingfluidandresidualoilmixtoformonephase.If theinterfacialtensioniszero,thenthecapillarynumberNVCbecomesinfiniteandthemicroscopic displacementefficiencyismaximized. Figure11.5isaschematicofamiscibleprocess.FluidAisinjectedintotheformationand mixeswiththecrudeoil,forminganoilbank.AmixingzonedevelopsbetweenfluidAandtheoil bankandwillgrowduetodispersion.FluidAisfollowedbyfluidB,whichismisciblewithfluid AbutnotgenerallymisciblewiththeoilandwhichismuchcheaperthanfluidA.Amixingzone willalsobecreatedatthefluidA–fluidBinterface.ItisimportantthattheamountoffluidAthatis injectedbelargeenoughthatthetwomixingzonesdonotcomeincontact.Ifthefrontofthefluid A–fluidBmixingzonereachestherearofthefluidAoilmixingzone,viscousfingeringoffluidB throughtheoilcouldoccur.Ontheotherhand,thevolumeoffluidAmustbekeptsmalltoavoid largeinjected-chemicalcosts. Consideramiscibleprocesswithn-decaneastheresidualoil,propaneasfluidA,andmethaneasfluidB.Thesystempressureandtemperatureare2000psiaand100°F,respectively.At Projection well Injection well Residual oil Fluid B Fluid A Oil bank Connate water Figure 11.5 Schematic of an enhanced oil recovery process requiring the injection of two fluids. 11.3 Tertiary Oil Recovery 415 theseconditions,bothn-decaneandpropaneareliquidsandarethereforemiscibleinallproportions.The system temperature and pressure indicate that any mixture of methane and propane wouldbeinthegasstate;therefore,themethaneandpropanewouldbemiscibleinallproportions. However,themethaneandn-decanewouldnotbemiscibleforsimilarreasons.Ifthepressure werereducedto1000psiaandthetemperatureheldconstant,thepropaneandn-decanewould againbemiscible.However,mixturesofmethaneandpropanecouldbelocatedinatwo-phase regionandwouldnotlendthemselvestoamiscibledisplacement.Notethat,inthisexample,the propaneappearstoactasaliquidwheninthepresenceofn-decaneandasagaswhenincontact withmethane.Itisthisuniquecapacityofpropaneandotherintermediaterangehydrocarbons thatleadstothemiscibleprocess. Thereare,ingeneral,twotypesofmiscibleprocesses.Thefirsttypeisreferredtoasthe single-contact miscible process and involves such injection fluids as liquefied petroleum gases (LPG)andalcohols.Theinjectedfluidsaremisciblewithresidualoilimmediatelyoncontact.The secondtypeisthemultiple-contact, or dynamic,miscibleprocess.Theinjectedfluidsinthiscase areusuallymethane,inertfluids,oranenrichedmethanegassupplementedwithaC2-C6fraction; thisfractionofalkaneshastheuniqueabilitytobehavelikealiquidoragasatmanyreservoirconditions.Theinjectedfluidandoilareusuallynotmiscibleonfirstcontactbutrelyonaprocessof chemicalexchangeoftheintermediatehydrocarbonsbetweenphasestoachievemiscibility.These processesarediscussedingreatdetailinothertexts.16–20,23 11.3.2.1 Single-Contact Miscible Processes Thephasebehaviorofhydrocarbonsystemscanbedescribedthroughtheuseofternarydiagrams suchasFig.11.6.Crudeoilphasebehaviorcantypicallyberepresentedreasonablywellbythree fractions of the crude. One fraction is methane (C1).A second fraction is a mixture of ethane throughhexane(C2-C6).Thethirdfractionistheremaininghydrocarbonspecieslumpedtogether andcalledC7+. Figure11.6illustratestheternaryphasediagramforatypicalhydrocarbonsystemwiththese threepseudocomponentsatthecornersofthetriangle.Thereareone-phaseandtwo-phaseregions (enclosedwithinthecurvedlineV0-C-L0)inthediagram.Theone-phaseregionmaybevaporor liquid(totheleftofthedashedlinethroughthecriticalpoint,C)orgas(totherightofthedashed linethroughthecriticalpoint).Agascouldbemixedwitheitheraliquidoravaporinappropriate percentagesandyieldamisciblesystem.However,whenliquidismixedwithavapor,oftenthe resultisacompositioninthetwo-phaseregion.Amixingprocessisrepresentedonaternarydiagramasastraightline.Forexample,ifcompositionsV and Garemixedinappropriateproportions, theresultingmixturewouldfallonthelineVG.IfcompositionsV and Laremixed,theresulting overallcompositionMwouldfallonthelineVLbutthemixturewouldyieldtwophasessincethe resultingmixturewouldfallwithinthetwo-phaseregion.Iftwophasesareformed,theircompositions,V1 and L1,wouldbegivenbyatielineextendedthroughthepointMtothephaseenvelope. ThepartofthephaseboundaryonthephaseenvelopefromthecriticalpointCtopointV0isthe dew-pointcurve.ThephaseboundaryfromCtoL0isthebubble-pointcurve.Theentirebubble point–dewpointcurveisreferredtoasthebinodal curve. Chapter 11 416 • Enhanced Oil Recovery C1 V0 V V1 M C G L0 C7+ L1 L C2 – C6 Figure 11.6 Ternary diagram illustrating typical hydrocarbon phase behavior at constant temperature and pressure. Theoil–LPG–drygassystemwillbeusedtoillustratethebehaviorofthefirst-contactmiscibleprocessonaternarydiagram.Figure11.7isaternarydiagramwiththepointsO, P, and V representingtheoil,LPG,anddrygas,respectively.TheoilandLPGaremiscibleinallproportions. Amixingzoneattheoil-LPGinterfacewillgrowasthefrontadvancesthroughthereservoir.At therearoftheLPGslug,thedrygasandLPGaremiscible,andamixingzonewillalsobecreated atthisinterface.Ifthedrygas–LPGmixingzoneovertakestheLPG–oilmixingzone,miscibility willbemaintained,unlessthecontactofthetwozonesyieldsmixturesinsidethetwo-phaseregion (seeFig.11.7,lineM0M1). Reservoirpressuressufficienttoachievemiscibilityarerequired.Thislimitstheapplication ofLPGprocessestoreservoirshavingpressuresatleastoftheorderof1500psia.Reservoirswith pressureslessthanthismightbeamenabletoalcoholflooding,anotherfirst-contactmiscibleprocess,sincealcoholstendtobesolublewithbothoilandwater(thedrivefluidinthiscase).The twomainproblemswithalcoholsarethattheyareexpensiveandtheybecomedilutedwithconnate waterduringafloodingprocess,whichreducesthemiscibilitywiththeoil.Alcoholsthathavebeen consideredareintheC1-C4 range. 11.3 Tertiary Oil Recovery 417 C1 V M0 P C7+ Figure 11.7 O M1 C2 – C6 Ternary diagram illustrating the single-contact miscible process. 11.3.2.2 Multiple-Contact Miscible Processes Multiple-contactordynamicmiscibleprocessesdonotrequiretheoilanddisplacingfluidtobe miscibleimmediatelyoncontactbutrelyonchemicalexchangebetweenthetwophasesformiscibilitytobeachieved.Figure11.8illustratesthehigh-pressure(lean-gas)vaporizing,orthedrygas miscibleprocess. Thetemperatureandpressureareconstantthroughoutthediagramatreservoirconditions. AvapordenotedbyVinFig.11.8,consistingmainlyofmethaneandasmallpercentageofintermediates,willserveastheinjectionfluid.TheoilcompositionisgivenbythepointO.Thefollowingsequenceofstepsoccursinthedevelopmentofmiscibility: 1. TheinjectionfluidVcomesincontactwithcrudeoilO.Theymix,andtheresultingoverall compositionisgivenbyM1.SinceM1islocatedinthetwo-phaseregion,aliquidphaseL1 andavaporphaseV1willformwiththecompositionsgivenbytheintersectionsofatieline throughM1,withthebubble-pointanddew-pointcurves,respectively. 2. TheliquidL1hasbeencreatedfromtheoriginaloilObythevaporizingofsomeofthelight components.SincetheoilOwasatitsresidualsaturationandwasimmobileduetotherelativepermeability,Kro,beingzero,whenaportionoftheoilisextracted,thevolume,and Chapter 11 418 • Enhanced Oil Recovery C1 V V1 M1 V2 V3 C L3 A C7+ Figure 11.8 L1 L2 O C2 – C6 Ternary diagram illustrating the multicontact dry gas miscible process. hencethesaturation,willdecreaseandtheoilwillremainimmobile.Thevaporphase,since Krgisgreaterthanzero,willmoveawayfromtheoilandbedisplaceddownstream. 3. ThevaporV1willcomeincontactwithfreshcrudeoilO,andagainthemixingprocesswill occur.Theoverallcompositionwillyieldtwophases,V2 and L2.Theliquidagainremainsimmobileandthevapormovesdownstream,whereitcomesincontactwithmorefreshcrude. 4. Theprocessisrepeatedwiththevapor-phasecompositionmovingalongthedew-pointcurve, V1-V2-V3,andsoon,untilthecriticalpoint,C,isreached.Atthispoint,theprocessbecomes miscible.Intherealcase,becauseofreservoirandfluidpropertyheterogeneitiesanddispersion,theremaybeabreakingdownandareestablishmentofmiscibility. Behindthemisciblefront,thevapor-phasecompositioncontinuallychangesalongthedewpointcurve.Thisleadstopartialcondensingofthevaporphasewiththeresultingcondensatebeing immobile,buttheamountofliquidformedwillbequitesmall.Theliquidphase,behindthemisciblefront,continuallychangesincompositionalongthebubblepoint.Whenalloftheextractable componentshavebeenremovedfromtheliquid,asmallamountofliquidwillbeleft,whichwill remainimmobile.Therewillbethesetwoquantitiesofliquidthatwillremainimmobileandnotbe recoveredbythemiscibleprocess.Inpractice,operatorshavereportedthatthevaporfronttravels anywherefrom20ftto40ftfromthewellborebeforemiscibilityisachieved. 11.3 Tertiary Oil Recovery 419 The high-pressure vaporizing process requires a crude oil with significant percentages of intermediatecompounds.Itistheseintermediatesthatarevaporizedandcombinedwiththeinjectionfluidtoformavaporthatwilleventuallybemisciblewiththecrudeoil.Thisrequirementof intermediatesmeansthattheoilcompositionmustlietotherightofatielineextendedthroughthe criticalpointonthebinodalcurve(seeFig.11.8).Acompositionlyingtotheleft,suchasdenoted bypointA,willnotcontainsufficientintermediatesformiscibilitytodevelop.Thisisduetothe factthattherichestvaporinintermediatesthatcanbeformedwillbeonatielineextendedthrough pointA.Clearly,thisvaporwillnotbemisciblewithcrudeoilA. Aspressureisreduced,thetwo-phaseregionincreases.Itisdesirable,ofcourse,tokeep thetwo-phaseregionminimalinsize.Asarule,pressuresoftheorderof3000psiaorgreater andanoilwithanAPIgravitygreaterthan35arerequiredformiscibilityinthehigh-pressure vaporizingprocess. Theenrichedgas-condensingprocessisasecondtypeofdynamicmiscibleprocess(Fig.11.9). Asinthehigh-pressurevaporizingprocess,wherechemicalexchangeofintermediatesisrequired formiscibility,miscibilityisdevelopedduringaprocessofexchangeofintermediateswiththeinjectionfluidandtheresidualoil.Inthiscase,however,theintermediatesarecondensedfromthe injectionfluidtoyielda“new”oil,whichbecomesmisciblewiththe“old”oilandtheinjectedfluid. C1 V1 V2 G C M1 L2 C7+ O L1 C2 – C6 Figure 11.9 Ternary diagram illustrating the multicontact enriched gas-condensing miscible process. 420 Chapter 11 • Enhanced Oil Recovery Thefollowingstepsoccurintheprocess(thesequenceofstepsissimilartothosedescribedforthe high-pressurevaporizingprocessbutcontainsomesignificantdifferences): 1. AninjectionfluidGrichinintermediatesmixeswithresidualoilO. 2. Themixture,givenbytheoverallcompositionM1,separatesintoavaporphase,V1, and a liquidphase,L1. 3. Thevapormovesaheadoftheliquidthatremainsimmobile.Theremainingliquid,L1,isthen contactedbyfreshinjectionfluid,G.Anotherequilibriumoccurs,andphaseshavingcompositionsV2 and L2areformed. 4. Theprocessisrepeateduntilaliquidisformedfromoneoftheequilibrationstepsthatis misciblewithG.Miscibilityisthensaidtohavebeenachieved. Ahead of the miscible front, the oil continually changes in composition along the bubble-point curve.Incontrasttothehigh-pressurevaporizingprocess,thereisthepotentialfornoresidualoil tobeleftbehindinthereservoiraslongasthereisasufficientamountofGinjectedtosupplythe condensingintermediates.Theenrichedgasprocessmaybeappliedtoreservoirscontainingcrude oilswithonlysmallquantitiesofintermediates.Reservoirpressuresareusuallyintherangeof 2000psiato3000psia. Theintermediatesareexpensive,andsousuallyadrygasisinjectedafterasufficientvolume ofenrichedgashasbeeninjected. 11.3.2.3 Inert Gas Injection Processes Theuseofinertgases,inparticularCO2 and N2,asinjectedfluidsinmiscibleprocesses,hasbecomeextremelypopular.TherepresentationoftheprocesswithCO2 or N2ontheternarydiagram isexactlythesameasthehigh-pressurevaporizingprocess,withtheexceptionthateitherCO2 or N2becomesacomponentandmethaneislumpedwiththeintermediates.Typicallytheone-phase regionislargestforCO2,withN2anddrygashavingaboutthesameone-phasesize.Thelargerthe one-phaseregion,themorereadilymiscibilitywillbeachieved.Miscibilitypressuresarelowerfor CO2,usuallyintheneighborhoodof1200psiato1500psia,whereasN2anddrygasyieldmuch highermiscibilitypressures(i.e.,3000psiaormore). ThecapacityofCO2tovaporizehydrocarbonsismuchgreaterthanthatofnaturalgas.It hasbeenshownthatCO2vaporizeshydrocarbonsprimarilyinthegasolineandgas-oilrange. ThiscapacityofCO2toextracthydrocarbonsistheprimaryreasonfortheuseofCO2 as an oil recoveryagent.ItisalsothereasonCO2requireslowermiscibilitypressuresthannaturalgas. ThepresenceofotherdiluentgasessuchasN2,methane,orfluegaswiththeCO2willraisethe miscibilitypressure.Themultiple-contactmechanismworksnearlythesamewithadiluentgas addedtotheCO2asitdoesforpureCO2.Frequently,anapplicationoftheCO2processinthe fieldwilltoleratehighermiscibilitypressuresthanwhatpureCO2wouldrequire.Ifthisisthe case,theoperatorcandilutetheCO2withotheravailablegas,raisingthemiscibilitypressurebut alsoreducingtheCO2requirements.DuetotherecentconsiderationtosequesterCO2because ofitscontributionstogreenhousegases,companiesmayfinditverydesirabletouseCO2 as a floodingagent. 11.3 Tertiary Oil Recovery 421 Thepressureatwhichmiscibilityisachievedisbestdeterminedbyconductingaseriesof displacementexperimentsinalong,slimtube.Aplotofoilrecoveryversusfloodingpressureis made,andtheminimummiscibilitypressureisdeterminedfromtheplot. 11.3.2.4 Problems in Applying the Miscible Process Becauseofdifferencesindensityandviscositybetweentheinjectedfluidandthereservoirfluid(s),themiscibleprocessoftensuffersfrompoormobility.Viscousfingeringandgravityoverride frequentlyoccur.Thesimultaneousinjectionofamiscibleagentandbrinemaytakeadvantageof thehighmicroscopicdisplacementefficiencyofthemiscibleprocessandthehighmacroscopic displacementefficiencyofawaterflood.However,theimprovementmaynotbeasgoodashoped forsincethemiscibleagentandbrinemayseparateduetodensitydifferences,withthemiscible agentflowingalongthetopoftheporousmediumandthebrinealongthebottom.Severalother variations of the simultaneous injection scheme may be attempted. These typically involve the injectionofamiscibleagentfollowedbybrineorthealteringofmiscibleagent-brineinjection. ThelattervariationhasbeennamedtheWAGprocess(discussedearlier)andhasbecomethemost popular.Abalancebetweenamountsofinjectedwaterandgashastobeachieved.Toomuchgas willleadtoviscousfingeringandgravityoverrideofthegas,whereastoomuchwatercouldleadto thetrappingofreservoiroilbythewater.Theadditionoffoamgeneratingsubstancestothebrine phasemayaidinreducingthemobilityofthegasphase. Operational problems involving miscible processes include transportation of the miscible floodingagent,corrosionofequipmentandtubing,andseparationandrecyclingofthemiscible floodingagent. 11.3.3 Chemical Flooding Processes Chemicalfloodingprocessesinvolvetheadditionofoneormorechemicalcompoundstoaninjectedfluideithertoreducetheinterfacialtensionbetweenthereservoiroilandinjectedfluidorto improvethesweepefficiencyoftheinjectedfluidbymakingitmoreviscous,therebyimproving themobilityratio.Bothmechanismsaredesignedtoincreasethecapillarynumber. Threegeneralmethodsaretypicallyincludedinchemicalfloodingtechnology.Thefirstis polymer flooding, in which a large macromolecule is used to increase the displacing fluid viscosity.Thisprocessleadstoimprovedsweepefficiencyinthereservoiroftheinjectedfluid.The remainingtwomethods,micellar-polymer flooding and alkaline flooding,makeuseofchemicals thatreducetheinterfacialtensionbetweenoilandadisplacingfluid.Thistextwillincludeafourth method—microbialflooding. 11.3.3.1 Polymer Processes The addition of large molecular weight molecules called polymers to an injected water can oftenincreasetheeffectivenessofaconventionalwaterflood.Polymersareusuallyaddedtothe waterinconcentrationsrangingfrom250to2000partspermillion(ppm).Apolymersolution ismoreviscousthanbrinewithoutpolymer.Inafloodingapplication,theincreasedviscosity willalterthemobilityratiobetweentheinjectedfluidandthereservoiroil.Theimprovedmo- 422 Chapter 11 • Enhanced Oil Recovery bilityratiowillleadtobetterverticalandarealsweepefficienciesandthushigheroilrecoveries.Polymershavealsobeenusedtoaltergrosspermeabilityvariationsinsomereservoirs.In thisapplication,polymersformagel-likematerialbycross-linkingwithotherchemicalspecies.Thepolymergelsetsupinlargepermeabilitystreaksanddivertstheflowofanyinjected fluidtoadifferentlocation. Twogeneraltypesofpolymershavebeenused.Thesearesyntheticallyproducedpolyacrylamides and biologically produced polysaccharides. Polyacrylamides are long molecules with a smalleffectivediameter.Thustheyaresusceptibletomechanicalshear.Highratesofflowthrough valveswillsometimesbreakthepolymerintosmallerentitiesandreducetheviscosityofthesolution.Areductioninviscositycanalsooccurasthepolymersolutiontriestosqueezethroughthe pore openings on the sand face of the injection well.A carefully designed injection scheme is necessary.Polyacrylamidesarealsosensitivetosalt.Largesaltconcentrations(i.e.,greaterthan 1–2wt%)tendtomakethepolymermoleculescurlupandlosetheirviscosity-buildingeffect. Polysaccharidesarelesssusceptibletobothmechanicalshearandsalt.Sincetheyareproducedbiologically,caremustbetakentopreventbiologicaldegradationinthereservoir.Asarule, polysaccharidesaremoreexpensivethanpolyacrylamides. Polymerfloodinghasnotbeensuccessfulinhigh-temperaturereservoirs.Neitherpolymer type has exhibited sufficiently long-term stability above 160°F in moderate-salinity or heavysalinitybrines. Polymerfloodinghasthebestapplicationinmoderatelyheterogeneousreservoirsandreservoirscontainingoilswithviscositieslessthan100centipoise(cp).Polymerprojectsmayfind somesuccessinreservoirshavingwidelydifferingproperties—thatis,permeabilitiesranging from20–2000millidarcies(md),insituoilviscositiesofupto100cp,andreservoirtemperaturesofupto200°F. Sincetheuseofpolymersdoesnotaffectthemicroscopicdisplacementefficiency,theimprovementinoilrecoverywillbeduetoimprovedsweepefficiencyoverwhatisobtainedduringa conventionalwaterflood.Typicaloilrecoveriesfrompolymerfloodingapplicationsareintherange of1%to5%oftheinitialoilinplace.Operatorsaremorelikelytohaveasuccessfulpolymerflood iftheystarttheprocessearlyintheproducinglifeofthereservoir. 11.3.3.2 Micellar-Polymer Processes Thebasicmicellar-polymerprocessusesasurfactanttolowertheinterfacialtensionbetweenthe injectedfluidandthereservoiroil.Asurfactantisasurface-activeagentthatcontainsahydrophobic(“dislikes”water)parttothemoleculeandahydrophilic(“likes”water)part.Thesurfactant migratestotheinterfacebetweentheoilandwaterphasesandhelpsmakethetwophasesmore miscible.Interfacialtensionscanbereducedfrom~30dynes/cm,foundintypicalwaterflooding applications,to10–4dynes/cm,withtheadditionofaslittleas0.1wt%to5.0wt%surfactantto water-oilsystems.Soapsanddetergentsusedinthecleaningindustryaresurfactants.Thesame principlesinvolvedinwashingsoiledlinenorgreasyhandsareusedin“washing”residualoiloff rockformations.Astheinterfacialtensionbetweenanoilphaseandawaterphaseisreduced,the capacityoftheaqueousphasetodisplacethetrappedoilphasefromtheporesoftherockmatrix 11.3 Tertiary Oil Recovery 423 increases. The reduction of interfacial tension results in a shifting of the relative permeability curvessothattheoilwillflowmorereadilyatloweroilsaturations. Whensurfactantsaremixedaboveacriticalsaturationinawater-oilsystem,theresultisa stablemixturecalledamicellar solution.Themicellarsolutionismadeupofstructurescalledmicroemulsions,whicharehomogeneous,transparent,andstabletophaseseparation.Theycanexist inseveralshapes,dependingontheconcentrationsofsurfactant,oil,water,andotherconstituents. Sphericalmicroemulsionshavetypicalsizerangesfrom10–6to10–4mm.Amicroemulsionconsists ofexternalandinternalphasessandwichedaroundoneormorelayersofsurfactantmolecules.The externalphasecanbeeitheraqueousorhydrocarboninnature,ascantheinternalphase. Solutionsofmicroemulsionsareknownbyseveralothernames,includingsurfactantsolutions, soluble oils, and micellar solutions. Figure 11.5 can be used to represent the micellarpolymerprocess.Acertainvolumeofthemicellarorsurfactantsolution,fluidA,isinjectedinto thereservoir.Thesurfactantsolutionisthenfollowedbyapolymersolution,fluidB,toprovide amobilitybufferbetweenthesurfactantsolutionandthedrivewater,whichisusedtopushthe entiresystemthroughthereservoir.Thepolymersolutionisdesignedtopreventviscousfingering ofthedrivewaterthroughthesurfactantsolutionasitstartstobuildupanoilbankaheadofit.As thesurfactantsolutionmovesthroughthereservoir,surfactantmoleculesareretainedontherock surface due to the process of adsorption. Often a preflush is injected ahead of the surfactant to preconditionthereservoirandreducethelossofsurfactantstoadsorption.Thispreflushcontains sacrificialagentssuchassodiumtripolyphosphate. Thereare,ingeneral,twotypesofmicellar-polymerprocesses.Thefirstusesalow-concentrationsurfactantsolution(lessthan2.5wt%)butalargeinjectedvolume(upto50%porevolume). Thesecondinvolvesahigh-concentrationsurfactantsolution(5wt%to12wt%)andasmallinjectedvolume(5%to15%porevolume).Eithertypeofprocesshasthepotentialofachievinglow interfacialtensionswithawidevarietyofbrinecrudeoilsystems. Whetherthelow-concentrationorthehigh-concentrationsystemisselected,thesystemis madeupofseveralcomponents.Themulticomponentfacetleadstoanoptimizationproblem,since many different combinations could be chosen. Because of this, a detailed laboratory screening procedureisusuallyundertaken.Thescreeningproceduretypicallyinvolvesthreetypesoftests: (1)phasebehaviorstudies,(2)interfacialtensionstudies,and(3)oildisplacementstudies. Phasebehaviorstudiesaretypicallyconductedinsmall(upto100ml)vialsinordertodeterminewhattype,ifany,ofmicroemulsionisformedwithagivenmicellar-crudeoilsystem.The salinityofthemicellarsolutionisusuallyvariedaroundthesaltconcentrationofthefieldbrine wheretheprocesswillbeapplied.Besidesthemicroemulsiontype,otherfactorsexaminedcould beoiluptakeintothemicroemulsion,easewithwhichtheoilandaqueousphasesmix,viscosityof themicroemulsion,andphasestabilityofthemicroemulsion. Interfacial tension studies are conducted with various concentrations of micellar solution componentstodetermineoptimalconcentrationranges.Measurementsareusuallymadewiththe spinningdrop,pendentdrop,orthesessiledroptechniques. Theoildisplacementstudiesarethefinalstepinthescreeningprocedure.Theyareusually conductedintwoormoretypesofporousmedia.Ofteninitialscreeningexperimentsareconducted 424 Chapter 11 • Enhanced Oil Recovery in unconsolidated sand packs and then in Berea sandstone. The last step in the sequence is to conducttheoildisplacementexperimentsinactualcoredsamplesofreservoirrock.Frequently, actualcoresamplesareplacedendtoendinordertoobtainacoreofreasonablelength,sincethe individualcoresamplesaretypicallyonly5–7in.long. Iftheoilrecoveriesfromtheoildisplacementtestswarrantfurtherstudyoftheprocess,the nextstepisusuallyasmallfieldpilotstudyinvolvinganywherefrom1to10acres. Themicellar-polymerprocesshasbeenappliedinseveralprojects.Theresultshavenotbeen veryencouraging.Theprocesshasdemonstratedthatitcanbeatechnicalsuccess,buttheeconomicsoftheprocesshasbeeneithermarginalorpoorinnearlyeveryapplication.19,20Asthepriceof oilincreases,themicellar-polymerprocesswillbecomemoreattractive. 11.3.3.3 Alkaline Processes Whenanalkalinesolutionismixedwithcertaincrudeoils,surfactantmoleculesareformed.When theformationofsurfactantmoleculesoccursinsitu,theinterfacialtensionbetweenthebrineand oilphasescouldbereduced.Thereductionofinterfacialtensioncausesthemicroscopicdisplacementefficiencytoincrease,therebyincreasingoilrecovery. Alkaline substances that have been used include sodium hydroxide, sodium orthosilicate, sodiummetasilicate,sodiumcarbonate,ammonia,andammoniumhydroxide.Sodiumhydroxide hasbeenthemostpopular.Sodiumorthosilicatehassomeadvantagesinbrineswithahighdivalent ioncontent. There are optimum concentrations of alkaline and salt and optimum pH, where the interfacialtensionvaluesexperienceaminimum.Findingtheserequiresascreeningprocedure similartotheonediscussedpreviouslyforthemicellar-polymerprocess.Whentheinterfacial tensionisloweredtoapointwherethecapillarynumberisgreaterthan10–5,oilcanbemobilizedanddisplaced. Severalmechanismshavebeenidentifiedthataidoilrecoveryinthealkalineprocess.These includethefollowing:loweringofinterfacialtension,emulsificationofoil,andwettabilitychanges intherockformation.Allthreemechanismscanaffectthemicroscopicdisplacementefficiency, andemulsificationcanalsoaffectthemacroscopicdisplacementefficiency.Ifawettabilitychange isdesired,ahigh(2.0–5.0wt%)concentrationofalkalineshouldbeused.Otherwise,concentrationsoftheorderof0.5–2.0wt%ofalkalineareused. Theemulsificationmechanismhasbeensuggestedtoworkbyeitheroftwomethods.The firstisbyforminganemulsion,whichbecomesmobileandlatertrappedindownstreampores. Theemulsion“blocks”thepores,whichtherebydivertsflowandincreasesthesweepefficiency. Thesecondmechanismisbyagainforminganemulsion,whichbecomesmobileandcarriesoil dropletsthatithasentrainedtodownstreamproductionsites. Thewettabilitychangesthatsometimesoccurwiththeuseofalkalineaffectrelativepermeabilitycharacteristics,whichinturnaffectmobilityandsweepefficiencies. Mobilitycontrolisanimportantconsiderationinthealkalineprocess,asitisinalltertiary processes.Often,itisnecessarytoincludepolymerinthealkalinesolutioninordertoreducethe tendencyofviscousfingeringtotakeplace. 11.3 Tertiary Oil Recovery 425 Notallcrudeoilsareamenabletoalkalineflooding.Thesurfactantmoleculesareformed withtheheavier,acidiccomponentsofthecrudeoil.Testshavebeendesignedtodeterminethe susceptibilityofagivencrudeoiltoalkalineflooding.Oneofthesetestsinvolvestitratingtheoil withpotassiumhydroxide(KOH).AnacidnumberisfoundbydeterminingthenumberofmilligramsofKOHrequiredtoneutralize1gofoil.Thehighertheacidnumber,themorereactivethe oilwillbeandthemorereadilyitwillformsurfactants.Anacidnumberlargerthan~0.2mgKOH suggestspotentialforalkalineflooding. Ingeneral,alkalineprojectshavebeeninexpensivetoconduct,butrecoverieshavenotbeen largeinthepastfieldpilots.19–20 11.3.3.4 Microbial Flooding Microbialenhancedoilrecovery(MEOR)floodinginvolvestheinjectionofmicroorganismsthat reactwithreservoirfluidstoassistintheproductionofresidualoil.TheUSNationalInstitutefor Petroleum and Energy Research (NIPER) maintains a database of field projects that have used microbialtechnology.TherehasbeensignificantresearchconductedonMEOR,butfewpilotprojectshavebeenconducted.TheOil and Gas Journal’s2012surveyreportednoongoingprojects intheUnitedStatesrelatedtothistechnology.24However,researchersinChinahavereportedmild successwithMEOR.25 TherearetwogeneraltypesofMEORprocesses—thoseinwhichmicroorganismsreact withreservoirfluidstogeneratesurfactantsorthoseinwhichmicroorganismsreactwithreservoirfluidstogeneratepolymers.Bothprocessesarediscussedhere,alongwithafewconcluding commentsregardingtheproblemswithapplyingthem.ThesuccessofMEORprocesseswillbe highly dependent on reservoir characteristics. MEOR systems can be designed for reservoirs that have either a high or low degree of channeling.Therefore, MEOR applications require a thoroughknowledgeofthereservoir.Mineralcontentofthereservoirbrinewillalsoaffectthe growthofmicroorganisms. Microorganismscanbereactedwithreservoirfluidstogenerateeithersurfactantsorpolymers inthereservoir.Onceeitherthesurfactantorpolymerhasbeenproduced,theprocessesofmobilizing andrecoveringresidualoilbecomesimilartothosediscussedwithregardtochemicalflooding. Most pilot projects have involved an application of the huff and puff or thermal-cycling processdiscussedwithregardtothermalflooding.Asolutionofmicroorganismsisinjectedalong with a nutrient—usually molasses.When the solution of microorganisms has been designed to reactwiththeoiltoformpolymers,theinjectedsolutionwillenterhigh-permeabilityzonesand reacttoformthepolymersthatwillthenactasapermeabilityreducingagent.Whenoilisproduced duringthehuffstage,oilfromlowerpermeabilityzoneswillbeproduced.Conversely,thesolution ofmicroorganismscanbedesignedtoreactwiththeresidualcrudeoiltoformasurfactant.The surfactantlowerstheinterfacialtensionofthebrine-watersystem,whichtherebymobilizesthe residualoil.Theoilisthenproducedinthehuffpartoftheprocess. Thereactionofthemicroorganismswiththereservoirfluidsmayalsoproducegases,suchas CO2, N2,H2,andCH4.Theproductionofthesegaseswillresultinanincreaseinreservoirpressure, whichwilltherebyenhancethereservoirenergy. 426 Chapter 11 • Enhanced Oil Recovery Sincemicroorganismscanbereactedtoformeitherpolymersorsurfactants,aknowledgeof thereservoircharacteristicsiscritical.Ifthereservoirisfairlyheterogeneous,thenitisdesirableto generatepolymersinsitu,whichcouldbeusedtodivertfluidflowfromhigh-tolow-permeability channels. If the reservoir has low injectivity, then using microorganisms that produced polymers couldbeverydamagingtotheflowoffluidsnearthewellbore.Henceathoroughknowledgeofthe reservoircharacteristics,particularlythoseimmediatelyaroundthewellbore,isextremelyimportant. Reservoir brines could inhibit the growth of the microorganisms.Therefore, some simple compatibilitytestscouldresultinusefulinformationastotheviabilityoftheprocess.Thesecan besimpletest-tubeexperimentsinwhichreservoirfluidsand/orrockareplacedinmicroorganism-nutrientsolutionsandgrowthandmetaboliteproductionofthemicroorganismsaremonitored. MEORprocesseshavebeenappliedinreservoirbrinesuptolessthan100,000ppm,rock permeabilitiesgreaterthan75md,anddepthslessthan6800ft.Thisdepthcorrespondstoatemperatureofabout75°C.MostMEORprojectshavebeenperformedwithlightcrudeoilshaving APIgravitiesbetween30and40.Theseshouldbeconsidered“ruleofthumb”criteria.Themost importantconsiderationinselectingamicroorganism-reservoirsystemistoconductcompatibility teststomakesurethatmicroorganismgrowthcanbeachieved. 11.3.3.5 Problems in Applying Chemical Processes Themaintechnicalproblemsassociatedwithchemicalprocessesincludethefollowing:(1)screeningofchemicalstooptimizethemicroscopicdisplacementefficiency,(2)contactingtheoilinthe reservoir, and (3) maintaining good mobility in order to lessen the effects of viscous fingering. Therequirementsforthescreeningofchemicalsvarywiththetypeofprocess.Obviously,asthe number of components increases, the more complicated the screening procedure becomes.The chemicalsmustalsobeabletotoleratetheenvironmentinwhichtheyareplaced.Hightemperature andsalinitymaylimitthechemicalsthatcouldbeused. Themajorproblemexperiencedinthefieldtodateinchemicalfloodingprocesseshasbeen the inability to contact residual oil. Laboratory screening procedures have developed micellarpolymersystemsthathavedisplacementefficienciesapproaching100%whensandpacksoruniformconsolidatedsandstonesareusedastheporousmedium.Whenthesamemicellar-polymer systemisappliedinanactualreservoirrocksample,however,theefficienciesareusuallylowered significantly.Thisisduetotheheterogeneitiesinthereservoirsamples.Whentheprocessisapplied tothereservoir,theefficienciesbecomeevenworse.Researchneedstobeconductedonmethodsto reducetheeffectoftherockheterogeneitiesandtoimprovethedisplacementefficiencies. Mobilityresearchisalsobeingconductedtoimprovedisplacementsweepefficiencies.Ifgood mobilityisnotmaintained,thedisplacingfluidfrontwillnotbeeffectiveincontactingresidualoil. Operationalproblemsinvolvetreatingthewaterusedtomakeupthechemicalsystems,mixingthechemicalstomaintainproperchemicalcompositions,pluggingtheformationwithparticular chemicals such as polymers, dealing with the consumption of chemicals due to adsorption andmechanicalshearandotherprocessingsteps,andcreatingemulsionsintheproductionfacilities.Researchtoaddresstheseoperationalproblemsisongoing.Despitetheseproblems,chemical floodingcanbeeffectiveintherightreservoirconditionsandinafavorableeconomicenvironment. 11.3 Tertiary Oil Recovery 11.3.4 427 Thermal Processes Primaryandsecondaryproductionfromreservoirscontainingheavy,low-gravitycrudeoilsisusuallyaverysmallfractionoftheinitialoilinplace.Thisisduetothefactthatthesetypesofoils are very thick and viscous and, as a result, do not migrate readily to producing wells. Figure 11.10showsatypicalrelationshipbetweentheviscosityofseveralheavy,viscouscrudeoilsand temperature. Ascanbeseen,viscositiesdecreasebyordersofmagnitudeforcertaincrudeoils,withanincreaseintemperatureof100°Fto200°F.Thissuggeststhat,ifthetemperatureofacrudeoilinthe reservoircanberaisedby100°Fto200°Foverthenormalreservoirtemperature,theoilviscosity willbereducedsignificantlyandwillflowmuchmoreeasilytoaproducingwell.Thetemperatureofareservoircanberaisedbyinjectingahotfluidorbygeneratingthermalenergyinsituby combustingtheoil.Hotwaterorsteamcanbeinjectedasthehotfluid.Threetypesofprocesses willbediscussedinthissection:steamcycling,steamdrive,andinsitucombustion.Inadditionto 100,000 10,000 1000 200 California crude Kinematic viscosity (cp) 100 50 20 10 5 Wyoming crude 2 Gulf coast crude 2400 Figure 11.10 0 120 160 200 240 280 320 460 Temperature (ºF) 400 440 Typical viscosity-temperature relationships for several crude oils. 480 428 Chapter 11 • Enhanced Oil Recovery theloweringofthecrudeoilviscosity,thereareothermechanismsbywhichthesethreeprocesses recoveroil.Thesemechanismswillalsobediscussed. Mostoftheoilthathasbeenproducedbytertiarymethodstodatehasbeenaresultofthermalprocesses.Thereisapracticalreasonforthis,aswellasseveraltechnicalreasons.Inorderto producemorethan1%to2%oftheinitialoilinplacefromaheavy-oilreservoir,thermalmethods have to be employed.As a result, thermal methods were investigated much earlier than either miscibleorchemicalmethods,andtheresultingtechnologywasdevelopedmuchmorerapidly.26,27 11.3.4.1 Steam-Cycling or Stimulation Process Thesteam-cycling,orstimulation,processwasdiscoveredbyaccidentintheMeneGrandeTar Sands,Venezuela,in1959.Duringasteam-injectiontrial,itwasdecidedtorelievethepressure fromtheinjectionwellbybackflowingthewell.Whenthiswasdone,averyhighoilproduction ratewasobserved.Sincethisdiscovery,manyfieldshavebeenplacedonsteamcycling. Thesteam-cyclingprocess,alsoknownasthesteamhuffandpuff,steamsoak,orcyclicsteam injection,beginswiththeinjectionof5000bblto15,000bblofhigh-qualitysteam.Thiscouldtakea periodofdaystoweekstoaccomplish.Thewellisthenshutin,andthesteamisallowedtosoakthe areaaroundtheinjectionwell.Thissoakperiodisfairlyshort,usuallyfrom1to5days.Theinjection wellisthenplacedonproduction.Thelengthoftheproductionperiodisdictatedbytheoilproduction ratebutcouldlastfromseveralmonthstoayearormore.Thecycleisrepeatedasmanytimesasis economicallyfeasible.Theoilproductionwilldecreasewitheachnewcycle. Mechanismsofoilrecoveryduetothisprocessinclude(1)reductionofflowresistancenear the wellbore by reducing the crude oil viscosity and (2) enhancement of the solution gas drive mechanismbydecreasingthegassolubilityinanoilastemperatureincreases. Often,inheavy-oilreservoirs,thesteamstimulationprocessisappliedtodevelopinjectivity aroundaninjectionwell.Onceinjectivityhasbeenestablished,thesteamstimulationprocessis convertedtoacontinuoussteam-driveprocess. Theoilrecoveriesobtainedfromsteamstimulationprocessesaremuchsmallerthantheoil recoveriesthatcouldbeobtainedfromasteamdrive.However,itshouldbeapparentthatthesteam stimulationprocessismuchlessexpensivetooperate.Thecyclicsteamstimulationprocessisthe most common thermal recovery technique.19,20,24 Recoveries of additional oil have ranged from 0.21bblto5.0bblofoilperbarrelofsteaminjected. 11.3.4.2 Steam-Drive Process Thesteam-driveprocessismuchlikeaconventionalwaterflood.Onceapatternarrangementis established, steam is injected into several injection wells while the oil is produced from other wells.Thisisdifferentfromthesteamstimulationprocess,wherebytheoilisproducedfromthe samewellintowhichthesteamisinjected.Asthesteamisinjectedintotheformation,thethermal energyisusedtoheatthereservoiroil.Unfortunately,someoftheenergyalsoheatsuptheentire environment,suchasformationrockandwater,andislost.Someenergyisalsolosttotheunderburdenandoverburden.Oncetheoilviscosityisreducedbytheincreasedtemperature,theoilcan flowmorereadilytotheproducingwells.Thesteammovesthroughthereservoirandcomesin 11.3 Tertiary Oil Recovery 429 contactwithcoldoil,rock,andwater.Asthesteamcontactsthecoldenvironment,itcondenses, andahotwaterbankisformed.Thishotwaterbankactsasawaterfloodandpushesadditionaloil totheproducingwells. Severalmechanismshavebeenidentifiedthatareresponsiblefortheproductionofoilfrom asteamdrive.Theseincludethermalexpansionofthecrudeoil,viscosityreductionofthecrude oil,changesinsurfaceforcesasthereservoirtemperatureincreases,andsteamdistillationofthe lighterportionsofthecrudeoil. Moststeamapplicationshavebeenlimitedtoshallowreservoirsbecause,asthesteamisinjected,itlosesheatenergyinthewellbore.Ifthewellisverydeep,allthesteamwillbeconverted toliquidwater. Steamdriveshavebeenappliedinmanypilotandfield-scaleprojectswithverygoodsuccess. Oil recoveries have ranged from 0.3 bbl to 0.6 bbl of oil per barrel of steam injected.A Steam injection Oil production SAGD process Steam chamber Steam injection Oil production Reservoir Figure 11.11 Schematic of the steam assisted gravity drainage process (courtesy Canadian Centre for Energy Information). 430 Chapter 11 • Enhanced Oil Recovery processthatwasdevelopedinthe1970sandhasbecomeincreasinglypopularisthesteamassisted gravitydrainage(SAGD)process.Thisprocessinvolvesthedrillingoftwohorizontalwells(see Fig.11.11)afewmetersapart.Steamisinjectedinthetopwellandheavyoil,asitheatsupfrom thesteam,drainsintothebottomwell.Theprocessworksbestinreservoirswithhighverticalpermeabilityandhasreceivedmuchattentionbycompanieswithheavy-oilresources.Therehavebeen manyapplicationsofthisprocessinCanadaandVenezuela.19,20,24 11.3.4.3 In Situ Combustion Earlyattemptsatinsitucombustioninvolvedwhatisreferredtoastheforwarddrycombustion process.Thecrudeoilwasigniteddownhole,andthenastreamofairoroxygen-enrichedairwas injectedinthewellwherethecombustionwasoriginated.Theflamefrontwasthenpropagated throughthereservoir.Largeportionsofheatenergywerelosttotheoverburdenandunderburden withthisprocess.Toreducetheheatlosses,areversecombustionprocesswasdesigned.Inreverse combustion,theoilisignitedasinforwardcombustionbuttheairstreamisinjectedinadifferent well.Theairisthen“pushed”throughtheflamefrontastheflamefrontmovesintheoppositedirection.Theprocesswasfoundtoworkinthelaboratory,butwhenitwastriedinthefieldonapilot scale,itwasneversuccessful.Itwasfoundthattheflamewouldbeshutoffbecausetherewasno oxygensupplyandthat,wheretheoxygenwasbeinginjected,theoilwouldself-ignite.Thewhole processwouldthenreverttoaforwardcombustionprocess. Whenthereversecombustionprocessfailed,anewtechniquecalledtheforwardwetcombustion process was introduced. This process begins as a forward dry combustion does, but oncetheflamefronthasbeenestablished,theoxygenstreamisreplacedbywater.Asthewater comesincontactwiththehotzoneleftbythecombustionfront,itflashestosteam,usingenergy that otherwise would have been wasted. The steam moves through the reservoir and aids the displacementofoil.Thewetcombustionprocesshasbecometheprimarymethodofconducting combustionprojects. Notallcrudeoilsareamenabletothecombustionprocess.Forthecombustionprocessto functionproperly,thecrudeoilhastohaveenoughheavycomponentstoserveasthesourceoffuel forthecombustion.UsuallythisrequiresanoiloflowAPIgravity.Astheheavycomponentsinthe oilarecombusted,lightercomponentsaswellasfluegasesareformed.Thesegasesareproduced withtheoilandraisetheeffectiveAPIgravityoftheproducedoil. Thenumberofinsitucombustionprojectshasdecreasedsincethe1980s.Environmental andotheroperationalproblemshaveprovedtobeexcessivelyburdensometosomeoperators.26–27 11.3.4.4 Problems in Applying Thermal Processes Themaintechnicalproblemsassociatedwiththermaltechniquesarepoorsweepefficiencies,loss ofheatenergytounproductivezonesunderground,andpoorinjectivityofsteamorair.Poorsweep efficienciesareduetothedensitydifferencesbetweentheinjectedfluidsandthereservoircrude oils.Thelightersteamorairtendstorisetothetopoftheformationandbypasslargeportionsof crudeoil.Datahavebeenreportedfromfieldprojectsinwhichcoringoperationshavefoundsignificantdifferencesinresidualoilsaturationsinthetopandbottompartsofthesweptformation. 11.3 Tertiary Oil Recovery 431 Research needs to be conducted on methods of reducing the tendency for the injected fluids to overridethereservoiroil.Techniquesinvolvingfoamsarebeingemployed. Largeheatlossescontinuetobeassociatedwiththermalprocesses.Thewetcombustionprocesshasloweredtheselossesforthehighertemperaturecombustiontechniques,butthelossesare severeenoughinmanyapplicationstoprohibitthecombustionprocess.Thelossesarenotaslarge withthesteamprocessesbecausetheytypicallyinvolvelowertemperatures.Thedevelopmentof afeasibledownholegeneratorwillsignificantlyreducethelossesassociatedwithsteam-injection processes. Thepoorinjectivityfoundinthermalprocessesislargelyaresultofthenatureofthereservoircrudeoils.Operatorshaveappliedfracturetechnologyinconnectionwiththeinjectionof fluidsinthermalprocesses.Thishashelpedinmanyreservoirs. Operational problems include the following: the formation of emulsions, the corrosion ofinjectionandproductiontubingandfacilities,andadverseeffectsontheenvironment.When emulsionsareformedwithheavycrudeoil,theyareverydifficulttobreak.Operatorsneedtobe preparedforthis.Inthehigh-temperatureenvironmentscreatedinthecombustionprocessesand whenwaterandstackgasesmixintheproductionwellsandfacilities,corrosionbecomesaserious problem.Specialwelllinersareoftenrequired.Stackgasesalsoposeenvironmentalconcernsin bothsteamandcombustionapplications.Stackgasesareformedwhensteamisgeneratedbyeither coal-oroil-firedgeneratorsand,ofcourse,duringthecombustionprocessasthecrudeisburned. 11.3.5 Screening Criteria for Tertiary Processes Alargenumberofvariablesareassociatedwithagivenoilreservoir—forinstance,pressureand temperature, crude oil type and viscosity, and the nature of the rock matrix and connate water. Becauseofthesevariables,noteverytypeoftertiaryprocesscanbeappliedtoeveryreservoir.An initialscreeningprocedurewouldquicklyeliminatesometertiaryprocessesfromconsiderationin particularreservoirapplications.Thisscreeningprocedureinvolvestheanalysisofbothcrudeoil andreservoirproperties.Thissectionpresentsscreeningcriteriaforeachofthegeneraltypesof processespreviouslydiscussedinthischapter,exceptmicrobialflooding.(AdiscussionofMEOR screeningcriteriaappearsinsection11.3.5.3.)Itshouldberecognizedthattheseareonlyguidelines.Ifaparticularreservoir-crudeoilapplicationappearstobeonaborderlinebetweentwodifferentprocesses,itmaybenecessarytoconsiderbothprocesses.Oncethenumberofprocesseshas beenreducedtooneortwo,adetailedeconomicanalysisshouldthenbeconducted. Somegeneralconsiderationscanbediscussedbeforetheindividualprocessscreeningcriteriaarepresented.First,detailedgeologicalstudyisusuallydesirable,sinceoperatorshavefound that unexpected reservoir heterogeneities have led to the failure of many tertiary field projects. Reservoirsthatwerefoundtobehighlyfaultedorfracturedtypicallyyieldpoorrecoveriesfrom tertiary processes. Second, some general comments pertaining to economics can also be made. Whenanoperatorisconsideringtertiaryoilrecoveryinparticularapplications,candidatereservoirsshouldcontainsufficientrecoverableoilandbelargeenoughfortheprojecttobepotentially profitable.Also,deepreservoirscouldinvolvelargedrillingandcompletionexpensesifnewwells aretobedrilled. Table 11.2 Screening Criteria for Tertiary Oil Recovery Processes Process Oil gravity (°API) Oil Oil viscosity saturation (cp) (%) Formation type Net thickness (ft) Average permeability (md) Depth (ft) Temp (°F) Miscible Hydrocarbon >35 <10 >30 Sandstoneorcarbonate 15–25 __a >4500 __a Carbondioxide >25 <12 >30 Sandstoneorcarbonate 15–25 __a >2000 __a Nitrogen >35 <10 >30 Sandstoneorcarbonate 15–25 a __ >4500 __a Polymer >25 5–125 __b Sandstonepreferred __a >20 <9000 <200 Surfactant-polymer >15 20–30 >30 Sandstonepreferred __a >20 <9000 <200 13–35 <200 __ b Sandstonepreferred a __ >20 <9000 <200 >10 >20 >40–50 Sandorsandstonewith highporosity >10 >50 500–5000 __a 10–40 <1000 >40–50 Sandorsandstonewith highporosity <10 >50 >500 __a Chemical Alkaline Thermal Steamflooding Combustion Notcriticalbutshouldbecompatible Tenpercentmobileabovewaterfloodresidualoil a b 11.4 Summary 433 11.3.5.1 Screening Criteria Table11.2containsthescreeningcriteriathathavebeencompiledfromtheliteratureforthemiscible,chemical,andthermaltechniques. Themiscibleprocessrequirementsarecharacterizedbyalow-viscositycrudeoilandathin reservoir.Alow-viscosityoilwillusuallycontainenoughoftheintermediate-rangecomponents forthemulticontactmiscibleprocesstobeestablished.Therequirementofathinreservoirreduces thepossibilitythatgravityoverridewilloccurandyieldsamoreevensweepefficiency. Ingeneral,thechemicalprocessesrequirereservoirtemperaturesoflessthan200°F,asandstonereservoir,andenoughpermeabilitytoallowsufficientinjectivity.Thechemicalprocesseswill workonoilsthataremoreviscousthanwhatthemiscibleprocessesrequire,buttheoilscannotbe soviscousthatadversemobilityratiosareencountered.Limitationsaresetontemperatureandrock typesothatchemicalconsumptioncanbecontrolledtoreasonablevalues.Hightemperatureswill degrademostofthechemicalsthatarecurrentlybeingusedintheindustry. Inapplyingthethermalmethods,itiscriticaltohavealargeoilsaturation.Thisisespecially pertinenttothesteamfloodingprocess,becausesomeoftheproducedoilwillbeusedonthesurfaceasthesourceoffueltofirethesteamgenerators.Inthecombustionprocess,crudeoilisused asfueltocompresstheairstreamonthesurface.Thereservoirshouldbeofsignificantthicknessin ordertominimizeheatlosstothesurroundings. 11.4 Summary Therecoveryofnearly70%to75%ofalltheoilthathasbeendiscoveredtodateisanattractive targetforEORprocesses.TheapplicationofEORtechnologytoexistingfieldscouldsignificantly increasetheworld’sprovenreserves.Severaltechnicalimprovementswillhavetobemade,however,beforetertiaryprocessesarewidelyimplemented.Theeconomicclimatewillalsohavetobe positivebecausemanyoftheprocessesareeithermarginallyeconomicalornoteconomicalatall. Steamfloodingandpolymerprocessesarecurrentlyeconomicallyviable.Incomparison,theCO2 processismorecostlybutgrowingmoreandmorepopular.Themicellar-polymerprocessiseven moreexpensive. Inarecentreport,theUSDepartmentofEnergystatedthatnearly40%ofallEORoilproduced intheUnitedStateswasduetothermalprocesses.28Mostoftherestisfromgasinjectionprocesses, eithergasfloodingorthemisciblefloodingprocesses.Chemicalflooding,althoughhighlyresearched inthe1980s,isnotcontributingmuch,mostlyduetothecostsassociatedwiththeprocesses.28 EORtechnologyshouldbeconsideredearlyintheproducinglifeofareservoir.Manyof theprocessesdependontheestablishmentofanoilbankinorderfortheprocesstobesuccessful. Whenoilsaturationsarehigh,theoilbankiseasiertoform.Itiscrucialforengineerstounderstand thepotentialofEORandthewayEORcanbeappliedtoaparticularreservoir. Asdiscussedattheendofthepreviouschapter,animportanttoolthattheengineershould usetohelpidentifythepotentialforanenhancedoilrecoveryprocess,eithersecondaryortertiary, iscomputermodelingorreservoirsimulation.Thereaderisreferredtotheliteratureiffurtherinformationisneeded.29–33 434 Chapter 11 • Enhanced Oil Recovery Problems 11.1 Conductabriefliteraturereviewtoidentifyrecentapplicationsofenhancedoilrecovery.Of thetertiaryrecoveryprocessesdiscussedinthechapter,arethereprocessesthatarereceivingmoreattentionthanothers?Why? 11.2 ReviewthemostrecentOil and Gas Journalsurveyofenhancedoilrecoveryprojects.Are therecountriesthataremoreactivethanothersinregardstoEORprojects?Why? 11.3 Howaretheworld’soilreservesaffectedbythepriceofoil? 11.4 Howhasthecontinueddevelopmentoftechniquessuchasfrackingandhorizontaldrilling affectedtheimplementationofEORprojects? References 1. Society of Petroleum Engineers E&P Glossary,SocietyofPetroleumEngineers,2009. 2. R.E.Terry,“EnhancedOilRecovery,”Encyclopedia of Physical Science and Technology,3rd ed.,AcademicPress,2003,503–18. 3. C.R.Smith,Mechanics of Secondary Oil Recovery,RobertE.KriegerPublishing,1966. 4. G.P.Willhite,Waterflooding,Vol.3,SocietyofPetroleumEngineers,1986. 5. F.F.Craig,The Reservoir Engineering Aspects of Waterflooding,SocietyofPetroleumEngineers,1993. 6. L.W.Lake,ed.,Petroleum Engineering Handbook,Vol.5,SocietyofPetroleumEngineers, 2007. 7. T.Ahmed,Reservoir Engineering Handbook,4thed.,GulfPublishingCo.,2010. 8. J.J.TaberandR.S.Seright,“HorizontalInjectionandProductionWellsforEORorWaterflooding,”presentedbeforetheSPEconference,Mar.18–20,1992,Midland,TX. 9. M.AlgharaibandR.Gharbi,“ThePerformanceofWaterFloodswithHorizontalandMultilateralWells,”Petroleum Science and Technology (2007),25,No.8. 10. PennStateEarthandMineralSciencesEnergyInstitute,“GasFloodingJointIndustryProject,”http://www2011.energy.psu.edu/gf 11. N.Ezekwe,Petroleum Reservoir Engineering Practice,PearsonEducation,2011. 12. J.R.Christensen,E.H.Stenby,andA.Skauge,“ReviewofWAGFieldExperience,”SPEREE (Apr.2001),97–106. 13. S. Kokal andA.Al-Kaabi, Enhanced Oil Recovery: Challenges and Opportunities, World PetroleumCouncil,2010. 14. G. Mortis, “Special Report: EOR/Heavy Oil Survey: CO2 Miscible, Steam Dominate EnhancedOilRecoveryProcesses,”Oil and Gas Jour.(Apr.2010),36–53. References 435 15. P.DiPietro,P.Balash,andM.Wallace,“ANoteonSourcesofCO2SupplyforEnhanced-OilRecoveryOperations,”SPE Economics and Management(Apr.2012). 16. H.K.vanPoollenandAssociates,Enhanced Oil Recovery,PennWellPublishing,1980. 17. D.W.GreenandG.P.Willhite,Enhanced Oil Recovery,Vol.6,SocietyofPetroleumEngineers,1998. 18. L.W.Lake,Enhanced Oil Recovery,PrenticeHall,1989(reprintedin2010). 19. J.Sheng,Modern Chemical Enhanced Oil Recovery,GulfProfessionalPublishing,2011. 20. V.Alvarado and E. Manrique, Enhanced Oil Recovery: Field Planning, and Development Strategies,GulfProfessionalPublishing,2010. 21. J.J.Taber,“DynamicandStaticForcesRequiredtoRemoveaDiscontinuousOilPhasefrom PorousMediaContainingBothOilandWater,”Soc. Pet. Engr. Jour.(Mar.1969),3. 22. G.L.Stegemeier,“MechanismsofEntrapmentandMobilizationofOilinPorousMedia,”Improved Oil Recovery by Surfactant and Polymer Flooding,ed.D.O.ShahandR.S.Schechter, AcademicPress,1977. 23. F.I.StalkupJr.,Miscible Displacement,SocietyofPetroleumEngineers,1983. 24. L.Koottungal,“2012WorldwideEORSurvey,”Oil and Gas Jour.(Apr.2,2012),41–55. 25. Q. Li, C. Kang, H.Wang, C. Liu, and C. Zhang, “Application of Microbial Enhanced Oil RecoveryTechniquetoDaqingOilfield,”Biochemical Engineering Jour.(2002),11,197–99. 26. M.Prats,Thermal Recovery,SocietyofPetroleumEngineers,1982. 27. T.C.Boberg,Thermal Methods of Oil Recovery,JohnWileyandSons,1988. 28. USOfficeofFossilEnergy,“EnhancedOilRecovery,”http://energy.gov/fe/science-innovation/ oil-gas/enhanced-oil-recovery 29. J.J.Lawrence,G.F.Teletzke,J.M.Hutfliz,andJ.R.Wilkinson,“ReservoirSimulationofGas InjectionProcesses,”paperSPE81459,presentedattheSPE13thMiddleEastOilShowand Conference,Apr.5–8,2003,Bahrain. 30. T.Ertekin,J.H.Abou-Kassem,andG.R.King,Basic Applied Reservoir Simulation,Vol.10, SocietyofPetroleumEngineers,2001. 31. J.Fanchi,Principles of Applied Reservoir Simulation,3rded.,Elsevier,2006. 32. C.C.MattaxandR.L.Dalton,Reservoir Simulation,Vol.13,SocietyofPetroleumEngineers, 1990. 33. M.Carlson,Practical Reservoir Simulation,PennWellPublishing,2006. This page intentionally left blank C H A P T E R 1 2 History Matching 12.1 Introduction Oneofthemostimportantjobfunctionsofthereservoirengineeristhepredictionoffutureproductionratesfromagivenreservoirorspecificwell.Overtheyears,engineershavedevelopedseveral methodstoaccomplishthistask.Themethodsrangefromsimpledecline-curveanalysistechniques tosophisticatedmultidimensional,multiflowreservoirsimulators.1–7Whetherasimpleorcomplex methodisused,thegeneralapproachtakentopredictproductionratesistocalculateproducing ratesforaperiodforwhichtheengineeralreadyhasproductioninformation.Ifthecalculatedrates matchtheactualrates,thecalculationisassumedtobecorrectandcanthenbeusedtomakefuture predictions.Ifthecalculatedratesdonotmatchtheexistingproductiondata,someoftheprocess parametersaremodifiedandthecalculationrepeated.Theprocessofmodifyingtheseparameters tomatchthecalculatedrateswiththeactualobservedratesisreferredtoashistory matching. Thecalculationalmethod,alongwiththenecessarydatausedtoconductthehistorymatch, isoftenreferredtoasamathematical model or simulator.Whendecline-curveanalysisisusedas thecalculationalmethod,theengineerisdoinglittlemorethancurvefitting,andtheonlydatathat arenecessaryaretheexistingproductiondata.However,whenthecalculationaltechniqueinvolves multidimensionalmassandenergybalanceequationsandmultiflowequations,alargeamountof dataisrequired,alongwithacomputertoconductthecalculations.Withthiscomplexmodel,the reservoirisusuallydividedintoagrid.Thisallowstheengineertousevaryinginputdata,suchas porosity,permeability,andsaturation,indifferentgridblocks.Thisoftenrequiresestimatingmuch ofthedata,sincetheengineerusuallyknowsdataonlyatspecificcoringsitesthatoccurmuchless frequentlythanthegridblocksusedinthecalculationalprocedure. Historymatchingcoversawidevarietyofmethods,rangingincomplexityfromasimple decline-curveanalysistoacomplexmultidimensional,multiflowsimulator.Thischapterwillbegin withadiscussionoftheleastcomplexmodel—thatofsimpledecline-curveanalysis.Thiswillprovideastartingpointforamoreadvancedmodelthatusesthezero-dimensionalSchilthuismaterial balanceequation,discussedinearlierchapters. 437 Chapter 12 438 12.2 • History Matching History Matching with Decline-Curve Analysis Decline-curve analysis is a fairly straightforward method of predicting the future production ofawell,usingonlytheproductionhistoryofthatwell.Thistypeofanalysishasalongtraditionintheoilindustryandremainsoneofthemostcommontoolsforforecastingoilandgas production.8–13Ingeneral,therearetwoapproachestodecline-curveanalysis:(1)curvefitting theproductiondatausingoneofthreemodelsdevelopedbyArps8and(2)type-curvematching usingtechniquesdevelopedbyFetkovich.10Thischapterwillpresentabriefintroductiontothe approachdevelopedbyArps. InChapter8,thenotionsofthetransienttimeandpseudosteady-statetimeperiodswere discussed.The reader will recall that the transient time during the production life of a well referstothetimebeforetheeffectsoftheouterboundaryhasbeenfeltbytheproducingfluid. Thepseudosteady-statetimeperiodreferstothetimethattheeffectsoftheouterboundary have been felt and that the reservoir pressure is dropping at a uniform rate throughout the drainagevolumeofthewell.Theoretically,theapproachbyArpsrequiresthattheproducing wellbeinthepseudosteady-statetimeperiodbothfortheproductionperiodinwhichtheengineerisattemptingtomodelandforthefutureprojectedproductionlifethattheengineeris attemptingtopredict.Arpspredictedthattheproductiondeclinefromawellwouldmodelone ofthreecurves(exponential,hyperbolic,orharmonicdecline)andcouldberepresentedbythe followingequation: 1 dq = bq d q dt (12.1) where q=flowrateattimet t=time b=empiricalconstantderivedfromproductiondata d=Arps’sdecline-curveexponent(exponential,d=0;hyperbolic,0<d<1;harmonic,d=1) Example12.1illustratesdecline-curveanalysisbyconsideringtheproductionfromawell andassumingthattheproductiondatafitanexponentialcurve.Thefollowingstepsareperformed: 1. Theproductionhistoryofagivenwellisobtainedandplottedagainsttime. 2. Anexponentiallineoftheformq = qi*exp(–b*t)isfittothedata. 3. Theequationisextrapolatedtodeterminefutureproductionofthewell. 12.2 History Matching with Decline-Curve Analysis 439 Well 15-1 60 1200 50 1000 40 800 × × 30 600 × 20 × 400 × × × 10 GOR, SCF/STB Oil rate, STB/day × Oil production GOR 200 1 2 3 4 5 6 7 8 Time, years Figure 12.1 Actual production and instantaneous GOR for history-matching problems. Example 12.1 Determining the Production Forecast for Well 15-1 Using the Production History Shown in Fig. 12.1 Given SeetheproductionhistoryshowninFig.12.1. Solution UsingMicrosoftExcel,estimatetheproductionandtimefromFig.12.1.PlottheminExceland fitanexponentialtrendlinetothedata.Createanewtable,addingvaluesfortimeinexcessofthe productionhistory,andcalculatevaluesfortheflowratebasedontheequationgivenbythetrend line.Plotthesevaluesnexttotheactualdata. Thereadercanseethesimplicityofdecline-curveanalysisinthesolutionofthisproblem. However,theengineer,inusingthistechniquetopredictfuturehydrocarbonrecoveries,needs tobeawareoftheassumptionsbuiltintotheapproach—themainonebeingthatthedrainage areaofthewellwillcontinuetoperformasithadduringthetimethatthehistoryisattempting tobematched.Engineers,whilecontinuingtousesimpledecline-curveanalysis,arebecoming 440 12.3 History Matching 441 increasinglyawarethatsophisticatedmodelsusingmassandenergybalanceequationsandcomputermodelingtechniquesaremuchmorereliablewhenpredictingreservoirperformance. 12.3 History Matching with the Zero-Dimensional Schilthuis Material Balance Equation 12.3.1 Development of the Model ThematerialbalanceequationspresentedinChapters3to7andChapter10donotyieldinformationonfutureproductionratesbecausetheequationsdonothaveatimedimensionassociatedwith them.Theseequationssimplyrelateaveragereservoirpressuretocumulativeproduction.Toobtain rateinformation,amethodisneededwherebytimecanberelatedtoeithertheaveragereservoir pressureorcumulativeproduction.InChapter8,single-phaseflowinporousmediawasdiscussed andequationsweredevelopedforseveralsituationsthatrelatedflowratetoaveragereservoirpressure.Itshouldbepossible,then,tocombinethematerialbalanceequationsofChapters3to7and 10withtheflowequationsfromChapter8inamodelorsimulatorthatwouldprovidearelationship forflowratesasafunctionoftime.Themodelwillrequireaccuratefluidandrockpropertydata andpastproductiondata.Onceamodelhasbeentestedforaparticularwellorreservoirsystem andfoundtoreproduceactualpastproductiondata,itcanbeusedtopredictfutureproductionrates. Theimportanceofthedatausedinthemodelcannotbeoveremphasized.Ifthedataarecorrect,the predictionofproductionrateswillbefairlyaccurate. 12.3.1.1 The Material Balance Part of the Model Theproblemconsideredinthischapterinvolvesavolumetric,internalgas-drivereservoir.InChapter10,severaldifferentmethodstocalculatetheoilrecoveryasafunctionofreservoirpressurefor thistypeofreservoirwerepresented.Fortheexampleinthischapter,theSchilthuismethodisused. ThereaderwillrememberthattheSchilthuismethodrequirespermeabilityratioversussaturation informationandthesolutionofEqs.(10.33),(10.40),and(10.41),writtenwiththetwo-phaseformationvolumefactor: R = Rso + kg μo Bo ko μg Bg N p Bo SL = Sw + (1 − Sw ) 1 − N Boi (10.33) (10.40) Np Bi + Bg ( R p − Rsoi ) N −1 = 0 Bt − Bti (10.41) Chapter 12 442 • History Matching 12.3.1.2 Incorporating a Flow Equation into the Model Theprocedurementionedintheprevioussectionyieldsoilandgasproductionasafunctionofthe averagereservoirpressure,butitdoesnotgiveanyindicationofthetimerequiredtoproducethe oilandgas.Tocalculatethetimeandrateatwhichtheoilandgasareproduced,aflowequation isneeded.ItwasfoundinChapter8thatmostwellsreachthepseudosteadystateafterflowing forafewhourstoafewdays.Anassumptionwillbemadethatthewellusedinthehistorymatch describedinthischapterhasbeenproducedforatimelongenoughforthepseudosteady-stateflow tobereached.Forthiscase,Eq.(8.45)canbeusedtodescribetheoilflowrateintothewellbore: 0.00708 ko h p − pwf qo = r μ o Bo ln e − 0.75 rw (8.45) Thisequationassumespseudosteady-state,radialgeometryforanincompressiblefluid.Thesubscript,o,referstooil,andtheaveragereservoirpressure, p, isthepressureusedtodeterminethe production,Np,intheSchilthuismaterialbalanceequation.Theincrementaltimerequiredtoproduceanincrementofoilforagivenpressuredropisfoundbysimplydividingtheincrementaloil recoverybytheratecomputedfromEq.(8.45)atthecorrespondingaveragepressure: Δt = ΔN p qo (12.2) Thetotaltimethatcorrespondstoaparticularaveragereservoirpressurecanbedeterminedby summingtheincrementaltimesforeachoftheincrementalpressuredropsuntiltheaveragereservoirpressureofinterestisreached. SinceEq.(12.2)requiresΔNpandtheSchilthuisequationdeterminesΔNp/N, N,theinitialoil inplace,mustbeestimated.InChapter6,section6.3,itwasshownthattheinitialoilinplacecould beestimatedfromthevolumetricapproachbytheuseofthefollowingequation: N= 7758 Ahφ (1 − Swi ) Boi (12.3) CombiningtheseequationswiththesolutionoftheSchilthuismaterialbalanceequationyieldsthe necessaryproductionratesofbothoilandgas. 12.3 History Matching 12.3.2 443 The History Match The reservoir model developed in the previous two sections will now be applied to historymatchingproductiondatafromawellinavolumetric,internalgas-drivereservoir.Actualoilproductionandinstantaneousgas-oilratiosforthefirst3yearsofthelifeofthewellareplottedin Fig.12.1.ThedatafortheproblemwereobtainedfrompersonnelattheUniversityofKansasand areusedherebypermission.14 Thewellislocatedinareservoirthatissandstoneandproducedfromtwozones,separated byathinshalesection,approximately1ftto2ftinthickness.Thereservoirisclassifiedasastratigraphictrap.Thetwoproducingzonesdecreaseinthicknessandpermeabilityindirectionswhereit isbelievedthatapinch-outoccurs.Permeabilityandporositydecreasetounproductivelimitsboth aboveandbelowtheproducingformation.Theinitialreservoirpressurewas620psia.Theaverage porosityandinitialwatersaturationvalueswere21.5%and37%,respectively.Theareadrained bythewellis40ac.Averagethicknessesandabsolutepermeabilitieswerereportedtobe17ftand 9.6mdforzone1and14ftand7.2mdforzone2.Laboratorydataforfluidviscosities,formation volumefactors,solutiongas-oilratio,oilrelativepermeability,andthegas-to-oilpermeabilityratio areplottedinFigs.12.2to12.6. 3.0 .012 .011 1.0 .010 Oil viscosity, cp 2.0 100 200 300 400 500 600 700 Pressure, psia Figure 12.2 Oil and gas viscosity for Schilthuis history-matching problem. 800 Gas viscosity, cp Oil and gas viscosity Oil and gas formation volume factors 1.12 280 1.10 240 1.09 200 1.08 160 1.07 120 1.06 80 1.05 40 1.04 100 200 300 400 500 600 700 Pressure, psia Figure 12.3 Oil and gas formation volume factor for Schilthuis history-matching problem. 444 Oil volume factor, bbl/st. tank bbl Reciprocal of gas volume factor, SCF/res bbl 1.11 Solution gas-oil ratio RSO Solubility of gas in oil, SCF/st. tank bbl 160 120 80 40 100 200 300 400 500 Pressure, psia Figure 12.4 Solution gas-oil ratio for Schilthuis history-matching problem. 445 600 700 1.0 Relative permeability to oil versus gas saturation 0.9 0.8 0.7 KRO = KO /K 0.6 0.5 0.4 0.3 0.2 0.1 0 0 0.05 0.10 0.15 0.20 0.25 0.30 Gas saturation, fraction pore space Figure 12.5 Oil relative permeability for Schilthuis history-matching problem. 446 0.35 9 8 7 6 5 4 3 2 10 9 8 7 6 5 4 3 2 1 0.05 0.10 0.15 0.20 0.25 0.30 0.35 0.10 0.15 0.20 0.25 0.30 0.35 9 8 7 6 5 4 3 KG /KO 2 10-1 9 8 7 6 5 4 3 2 10-2 9 8 7 6 5 4 3 2 10-3 9 8 7 6 5 4 3 2 10-4 0.05 Gas saturation, fraction pore space Figure 12.6 Permeability ratio for Schilthuis history-matching problem. 447 Table 12.1 Excel Functions Used to Calculate Fluid Property Data for the Schilthuis HistoryMatching Problem Table 12.2 Excel Functions Used to Calculate Oil Relative Permeability Curve in the Schilthuis History-Matching Problem 448 12.3 History Matching 449 12.3.2.1 Solution Procedure Oneofthefirststepsinattemptingtoperformthehistorymatchistoconvertthefluidproperty dataprovidedinFigs.12.2to12.4toamoreusableform.Thisisdonebysimplyregressingthe datatocreateExcelfunctionsinMicrosoftExcel’sVisualBasicEditorforeachparameter—for example,oilandgasviscosityasafunctionofpressure.Theresultingfunctionscanbefoundin theprogramlistinginTable12.1.Thetwopermeabilityrelationshipsalsoneedtoberegressed foruseintheexample. Boththerelativepermeabilitytooilandthepermeabilityratiocanbeexpressedasfunctions ofgassaturation.TheseExcelfunctionsarestructuredinadifferentmannerfromthefluidproperty equations.Theconstantsfortheregressedequationsareplacedinanarray,showninTables12.2 and12.3,andaregressionisperformedbetweeneachsetofpoints.Theserelationshipsarehandled thiswaytofacilitatemodificationstotheequationsusedintheprogramifnecessary. WiththedataofFigs.12.2to12.6expressedinequationformat,thehistorymatchisnow readytobeexecuted.AnexampleoftheExcelworksheetisshowninTable12.4. The Excel sheet is laid out with the reservoir variables such as initial pressure, wellhead flowingpressure,reservoirarea,andsoonshownatthetopofthepage.Directlybelowarethe zone-specificdataofheight,initialhydrocarboninplace,andpermeability.Thosevaluesaretotaledto provideavaluefortheentirewell.Belowarethereservoirpropertiesateachaveragewellpressure in10-psiincrements.Totherightaretheactualproductionvaluesforthewells,andacomparison Table 12.3 Excel Functions Used to Calculate Gas to Oil Permeability Ratio Curve in the Schilthuis History-Matching Problem Table 12.4 Excel Worksheet Used in the Schilthuis History-Matching Problem 450 12.3 History Matching 451 betweenactualandcalculatedisshowninthegraphinthebottomcorner.Theequationsforeach ofthecellsareshowninTable12.5. The sheet requires a user-specified delNpguess value in order to determine the reservoir propertiesatagivenpressure.Oncethosevaluesaredetermined,thesheetautomaticallycalculates anewdelNpandanNpforthatpressure.ThedelNpguesswillneedtobeiterateduntilitisequalto delNp.Toaidinthis,thecheckcolumnwascreated.Attheendofthecheckcolumnisacellwith thesumofthecheckvalues.UsingExcel’sbuilt-insolvertool,thatcellcanbeiterativelysolved foraminimumvaluebyadjustingthedelNpguessforeachpressureincrement.Thisallowsthe usertorapidlysolvethesetofequationsintheSchilthuisbalanceandgettheresultatthatsetof conditions. 12.3.2.2 Discussion of History-Matching Results When the program is executed using the original data given in the problem statement as input, theoilproductionrateandR,orinstantaneousGOR,valuesobtainedresultintheplotsshownin Fig.12.7.Noticethatthecalculatedoilproductionrates,showninFig.12.7(a),beginhigherthan theactualratesanddecreasefasterwithtimeorwithagreaterslope.Thecalculatedinstantaneous GORvaluesarecomparedwiththeactualGORvaluesinFig.12.7(b)andfoundtobemuchlower thantheactualvalues. Atthispoint,itisnecessarytoaskhowthecalculatedinstantaneousGORvaluescouldbe raisedinorderforthemtomatchtheactualvalues.AnexaminationofEq.(10.33)suggeststhat Risafunctionoffluidpropertydataandtheratioofgas-to-oilpermeabilities.Tocalculatehigher valuesforR,eitherthefluidpropertydataorthepermeabilityratiodatamustbemodified.Becausefluidpropertydataarereadilyandaccuratelyobtainedandthepermeabilitiescouldchange significantlyinthereservoirowingtodifferentrockenvironments,itseemsjustifiedtomodify thepermeabilityratiodata.Itisoftenthecasewhenconductingahistorymatchthatanengineerwillfinddifferencesbetweenlaboratory-measuredpermeabilityratiosandfield-measured Table 12.5 Equations Used in the Schilthuis History-Matching Problem 90 80 Oil production, STB/day 70 60 50 40 30 20 Actual Q Calculated Q 10 0 0 1 2 Time, years 3 4 (a) Oil production rate 800 Gas-oil ratio, SCF/STB 700 600 500 400 300 200 Actual GOR Calculated GOR 100 0 0 1 2 Time, years (b) Instantaneous GOR Figure 12.7 Schilthuis history match using original data. 452 3 4 12.3 History Matching 453 permeabilityratios.Mueller,Warren,andWestshowedthatoneofthemainreasonsforthediscrepancybetweenlaboratorykg/kovaluesandfield-measuredvaluescanbeexplainedbytheunequalstagesofdepletioninthereservoir.15Forthesamereason,fieldinstantaneousGORvalues seldomshowtheslightdeclinepredictedintheearlystagesofdepletionand,conversely,usually showariseingas-oilratioatanearlierstageofdepletionthantheprediction.Whereasthetheoreticalpredictionsassumeanegligible(actuallyzero)pressuredrawdown,sothatthesaturations arethereforeuniformthroughoutthereservoir,actualwellpressuredrawdownswilldepletethe reservoir in the vicinity of the wellbore in advance of areas further removed. In development programs,somewellsareoftencompletedyearsbeforeotherwells,anddepletionisnaturally furtheradvancedintheareaoftheolderwells,whichwillhavegas-oilratiosconsiderablyhigher thanthenewerwells.Andevenwhenallwellsarecompletedwithinashortperiod,whenthe formationthicknessvariesandallwellsproduceatthesamerate,thereservoirwillbedepleted fasterwhentheformationisthinner.Finally,whenthereservoircomprisestwoormorestrataof differentspecificpermeabilities,eveniftheirrelativepermeabilitycharacteristicsarethesame, the strata with higher permeabilities will be depleted before those with lower permeabilities. Since all these effects are minimized in high-capacity formations, closer agreement between field and laboratory data can be expected for higher capacity formations. On the other hand, high-capacity formations tend to favor gravity segregation. When gravity segregation occurs andadvantageistakenofitbyshuttinginthehigh-ratiowellsorworkingoverwellstoreduce theirratios,thefield-measuredkg/kovalueswillbelowerthanthelaboratoryvalues.Thusthe laboratorykg/kovaluesmayapplyateverypointinareservoirwithoutgravitysegregation,and yetthefieldkg/kovalueswillbehigherowingtotheunequaldepletionofthevariousportionsof thereservoir. Thefollowingprocedureisusedtogeneratenewpermeabilityratiovaluesfromtheactual productiondata: 1. PlottheactualRvaluesversustimeanddeterminearelationshipbetweenRandtime. 2. Chooseapressureanddeterminethefluidpropertydataatthatpressure.Fromthechosen pressureandtheoutputdatainTable12.4,findthetimethatcorrespondswiththechosen pressure. 3. Fromtherelationshipfoundinstep1,calculateRforthetimefoundinstep2. 4. WiththevalueofRfoundinstep3andthefluidpropertydatafoundinstep2,rearrangeEq. (10.33)andcalculateavalueofthepermeabilityratio. 5. Fromthepressurechoseninstep2andfromtheNpvaluescalculatedfromthechosenpressure,calculatethevalueofthegassaturationthatcorrespondswiththecalculatedvalueof thepermeabilityratio. 6. Repeatsteps2through5forseveralpressures.Theresultwillbeanewpermeabilityratio– gassaturationrelationship. InExcel,thesolutionresemblesTable12.6. Table 12.6 Excel Worksheet Illustrating the Calculation of the New Permeability Ratio 454 12.3 History Matching 455 Thereadershouldrealizethatinsteps2and5theoriginalpermeabilityratiowasusedtogeneratethedataofTable12.4.Thissuggeststhatthenewpermeabilityratio–gassaturationrelationship couldbeinerrorbecauseitisbasedonthedataofTable12.4andthat,tohaveamorecorrectrelationship,itmightbenecessarytorepeattheprocedure.Thequalityofthehistorymatchobtainedwiththe newpermeabilityratiovalueswilldictatewhetherthisiterativeprocedureshouldbeusedingeneratingthenewpermeabilityratio–gassaturationrelationship.Thenewpermeabilityratiosdetermined fromtheprevioussix-stepprocedureareplottedwiththeoriginalpermeabilityratiosinFig.12.8. Itisnownecessarytoregressthenewpermeabilityratio–gassaturationrelationshipandinputthenewdataintotheExcelworksheetbeforethecalculationcanbeexecutedagaintoobtaina newhistorymatch.Whenthisisdone,thecalculationyieldstheresultsplottedinFig.12.9. Thenewpermeabilityratiodatahassignificantlyimprovedthematchoftheinstantaneous GORvalues,ascanbeseeninFigure12.9(b).However,theoilproductionratesarestillnotagood match.Infact,thenewpermeabilityratiodatahaveyieldedasteeperslopeforthecalculatedoil rates,asshowninFigure12.9(a),thanwhatisobservedinFigure12.7(a)fromtheoriginaldata.A lookatthecalculationschemehelpsexplaintheeffectofthenewpermeabilityratiodata. BecausethenewvaluesofinstantaneousGORwerecalculatedwiththenewpermeability ratiodata,whichinturnweredeterminedbyusingEq.(10.33)andtheactualGORvalues,itshould beexpectedthatthecalculatedGORvalueswouldmatchtheactualGORvalues.Theflowrate calculation,whichinvolvesEq.(8.45),doesnotusethepermeabilityratio,sothemagnitudeof theflowrateswouldnotbeexpectedtobeaffectedbythenewpermeabilityratiodata.However, thetimecalculationdoesinvolveNp,whichisafunctionofthepermeabilityratiointheSchilthuis materialbalancecalculation.Therefore,therateatwhichtheflowratesdeclinewillbealteredwith thenewpermeabilityratiodata. Toobtainamoreaccuratematchofoilproductionrates,itisnecessarytomodifyadditional data.Thisraisesthequestion,whatotherdatacanbejustifiablychanged?Itwasarguedthatitwas notjustifiabletomodifythefluidpropertydata.However,thefluidpropertydataand/orequations shouldbecarefullycheckedforpossibleerrors.Inthiscase,theequationswerecheckedbycalculatingvaluesofBo, Bg, Rso, μo, and μgatseveralpressuresandcomparingthemwiththeoriginal data.Thefluidpropertyequationswerefoundtobecorrectandaccurate.Otherassumedreservoir properties that could be in error include the zone thicknesses and absolute permeabilities. The thicknesses are determined from logging and coring operations from which an isopach map is created.Absolutepermeabilitiesaremeasuredfromasmallsampleofacoretakenfromalimited numberoflocationsinthereservoir.Thenumberofcoringlocationsislimitedlargelybecauseof thecostsinvolvedinperformingthecoringoperations.Althoughtheactualmeasurementofboth thethicknessandpermeabilityfromcoringmaterialishighlyaccurate,errorsareintroducedwhen onetriestoextrapolatethemeasuredinformationtotheentiredrainageareaofaparticularwell. Forinstance,whenconstructingtheisopachmapforthezonethickness,youneedtomakeassumptionsregardingthecontinuityofthezoneinbetweencoringlocations.Theseassumptionsmayor maynotbecorrect.Becauseofthepossibleerrorsintroducedindeterminingaveragevaluesfor thethicknessandpermeabilityforthewell-drainagearea,varyingtheseparametersandobserving theeffectofourhistorymatchisjustified.Intheremainderofthissection,theeffectofchanging 9 8 7 6 5 4 3 2 10 9 8 7 6 5 4 3 2 1 0.05 0.10 0.15 0.20 0.25 0.30 0.35 9 8 7 6 5 4 3 KG /KO 2 10-1 9 8 7 6 5 4 3 2 10-2 9 8 7 6 5 4 3 2 10-3 9 8 7 6 5 4 3 2 Original data First iteration 10-4 0.05 0.10 0.15 0.20 0.25 0.30 0.35 Gas saturation, fraction pore space Figure 12.8 First iteration of permeability ratio for history-matching problem. 456 90 80 Oil production, STB/day 70 60 50 40 30 20 Actual Q Calculated Q 10 0 0 1 2 Time, years 3 4 (a) Oil production rate 800 Gas-oil ratio, SCF/STB 700 600 500 400 300 200 Actual GOR Calculated GOR 100 0 0 1 2 Time, years 3 (b) Instantaneous GOR Figure 12.9 History match after modifying permeability ratio values. 457 4 Chapter 12 458 • History Matching theseparametersonthehistory-matchingprocessisexamined.Table12.7containsasummaryof thecasesthatarediscussed. Incase3,thethicknessesofbothzoneswereadjustedtodeterminetheeffectonthehistory match.Sincethecalculatedflowratesarehigherthantheactualflowrates,thethicknesseswere reduced. Figure 12.10 shows the effect on oil producing rate and instantaneous GOR when the thicknessesarereducedbyabout20%. By reducing the thicknesses, the calculated oil production rates are shifted downward, as showninFigure12.10(a). Thisyieldsagoodmatchwiththeearlydatabutnotwiththelaterdata,becausethecalculatedvaluesdeclineatamuchmorerapidratethantheactualdata.ThecalculatedinstantaneousGOR valuesstillcloselymatchtheactualGORvalues.Theseobservationscanbesupportedbynoting thatthezonethicknessentersintothecalculationschemeintwoplaces.Oneisinthecalculation forN,theinitialoilinplace,whichisperformedbyusingEq.(12.3).ThenNismultipliedbyeach oftheΔNp/NvaluesdeterminedintheSchilthuisbalance.Thesecondplacethethicknessisusedis intheflowequation,Eq.(8.45),whichisusedtocalculateqo.TheinstantaneousGORvaluesare notaffectedbecauseneitherthecalculationforNnorthecalculationforqoisusedinthecalculation forinstantaneousGORorR.However,theoilflowrateisdirectlyproportionaltothethickness,so asthethicknessisreduced,theflowrateisalsoreduced.Atfirstglance,itappearsthatthedecline rateoftheflowratewouldbealtered.Butuponfurtherstudy,itisfoundthatalthoughtheflow rateisobviouslyafunctionofthethickness,thetimeisnot.Tocalculatethetime,anincremental ΔNpisdividedbytheflowratecorrespondingwiththatincrementalproduction.SincebothNp and qoaredirectlyproportionaltothethickness,thethicknesscancelsout,therebymakingthetime independentofthethickness.Insummary,thenetresultofreducingthethicknessisasfollows: (1)themagnitudeoftheoilflowrateisreduced,(2)theslopesoftheoilproductionandinstantaneousGORcurvesarenotaltered,and(3)theinstantaneousGORvaluesarenotaltered. Todeterminetheeffectonthehistorymatchofvaryingtheabsolutepermeabilities,thepermeabilitieswerereducedbyabout20%incase4.Figure12.11showstheoilproductionratesand theinstantaneousGORplotsforthisnewcase.Thequalityofthematchofoilproductionrateshas improved,butthequalityofthematchoftheinstantaneousGORvalueshasdecreased.Again,if Table 12.7 Description of Cases Case number Parameter varied from original data 1 None 2 Permeabilityratio 3 Sameascase2pluszonethickness 4 Sameascase2plusabsolutepermeability 5 Sameascase2pluszonethicknessandabsolute permeability 6 Aseconditerationonthepermeabilityratiodatapluszone thicknessandabsolutepermeability 70 Oil production, STB/day 60 50 40 30 20 Actual Q Calculated Q 10 0 0 1 2 Time, years 3 4 (a) Oil production rate 800 Gas-oil ratio, SCF/STB 700 600 500 400 300 200 Actual GOR Calculated GOR 100 0 0 1 2 Time, years 3 4 (b) Instantaneous GOR Figure 12.10 History match of case 3. Case 3 used the new permeability ratio data and reduced zone thicknesses. 459 70 Oil production, STB/day 60 50 40 30 20 Actual Q Calculated Q 10 0 0 1 2 Time, years 3 4 (a) Oil production rate 800 Gas-oil ratio, SCF/STB 700 600 500 400 300 200 Actual GOR Calculated GOR 100 0 0 1 2 Time, years 3 4 (b) Instantaneous GOR Figure 12.11 History match of case 4. Case 4 used the new permeability ratio data and reduced absolute permeabilities. 460 12.3 History Matching 461 theequationsinvolvedareexamined,anunderstandingofhowchangingtheabsolutepermeabilitieshasaffectedthehistorymatchcanbeobtained. Equation(8.45)suggeststhattheoilflowrateisdirectlyproportionaltotheeffectivepermeabilitytooil,ko: ko = krok (12.4) Equation(12.4)showstherelationshipbetweentheeffectivepermeabilitytooilandtheabsolute permeability,k.CombiningEqs.(8.45)and(12.4),itcanbeseenthattheoilflowrateisdirectly proportionaltotheabsolutepermeability.Therefore,whentheabsolutepermeabilityisreduced, theoilflowrateisalsoreduced.Sincethetimevaluesareafunctionofqo,thetimevaluesarealso affected.ThemagnitudeoftheinstantaneousGORvaluesisnotafunctionoftheabsolutepermeability,sinceneithertheeffectivenortheabsolutepermeabilitiesareusedintheSchilthuismaterial balancecalculation.However,thetimevaluesaremodified,sotheslopeofboththeoilproduction rateandtheinstantaneousGORcurvesarealtered.Thisisexactlywhatshouldhappeninorderto obtainabetterhistorymatchoftheoilproductionvalues.However,althoughithasimprovedthe oilproductionhistorymatch,theinstantaneousGORmatchhasbeenmadeworse.Byreducingthe absolutepermeabilities,ithasbeenfoundthat(1)themagnitudeoftheoilflowratesarereduced, (2)themagnitudeoftheinstantaneousGORvaluesarenotchanged,and(3)theslopesofboththe oilproductionandinstantaneousGORcurvesarealtered. Bymodifyingthezonethicknessesandabsolutepermeabilities,themagnitudeoftheoilflow ratesandtheslopeoftheoilflowratecurvecanbemodified.Also,whileadjustingtheoilflowrate, slightchangesintheslopeoftheinstantaneousGORcurveareobtained.Incase5,boththezone thicknessandtheabsolutepermeabilityarechangedinadditiontousingthenewpermeabilityratio data.Figure12.12containsthehistorymatchforcase5.AscanbeseeninFigure12.12(a),the calculatedoilflowratesareanexcellentmatchtotheactualfieldoilproductionvalues.Thematch ofinstantaneousGORvalueshasworsenedfromcases2to4butisstillmuchimprovedoverthe matchincase1,whichwasobtainedbyusingtheoriginalpermeabilityratiodata. Aseconditerationofthepermeabilityratiovaluesmaybenecessary,dependingonthequality ofthefinalhistorymatchthatisobtained.Thisisbecausetheprocedureusedtoobtainthenewpermeabilityratiodatainvolvesusingtheoldpermeabilityratiodata.ThecalculatedinstantaneousGOR valuesdonotmatchtheactualfieldGORvaluesverywell,soaseconditerationofthepermeability ratiovaluesiswarranted.Followingtheprocedureofobtainingnewpermeabilityratiodatainconjunctionwiththeresultsofcase5,asecondsetofnewpermeabilityratiosisobtained.Thissecondset isplottedinFigure12.13,alongwiththeoriginaldataandthefirstsetusedincases2to5. By using the permeability ratio data from the second iteration and by adjusting the zone thicknessesandabsolutepermeabilitiesasneeded,theresultsshowninFigure12.14areobtained. ItcanbeseenthatthequalityofthehistorymatchforboththeoilproductionrateandtheinstantaneousGORvaluesisverygood.WhenahistorymatchisobtainedthatmatchesboththeoilproductionandinstantaneousGORcurvesthiswell,themodelcanbeusedwithconfidencetopredict futureproductioninformation. 70 Oil production, STB/day 60 50 40 30 20 Actual Q Calculated Q 10 0 0 1 2 Time, years 3 4 (a) Oil production rate 800 Gas-oil ratio, SCF/STB 700 600 500 400 300 200 Actual GOR Calculated GOR 100 0 0 1 2 Time, years 3 4 (b) Instantaneous GOR Figure 12.12 History match of case 5. Case 5 used the new permeability ratio data and modified zone thicknesses and absolute permeabilities. 462 9 8 7 6 5 4 3 2 10 9 8 7 6 5 4 3 2 1 0.05 0.10 0.15 0.20 0.25 0.30 0.35 9 8 7 6 5 4 3 KG /KO 2 10-1 9 8 7 6 5 4 3 2 10-2 9 8 7 6 5 4 3 2 10-3 9 8 7 6 5 4 3 Original data First iteration Second iteration 2 10-4 0.05 0.10 0.15 0.20 0.25 0.30 0.35 Gas saturation, fraction pore space Figure 12.13 Second iteration of permeability ratios for the history-matching problem. 463 70 Oil production, STB/day 60 50 40 30 20 Actual Q Calculated Q 10 0 0 1 2 Time, years 3 4 (a) Oil production rate 800 Gas-oil ratio, SCF/STB 700 600 500 400 300 200 Actual GOR Calculated GOR 100 0 0 1 2 Time, years 3 4 (b) Instantaneous GOR Figure 12.14 History match of case 6. Case 6 used permeability ratio data from a second iteration and modified zone thicknesses and absolute permeabilities. 464 12.3 History Matching 465 Table 12.8 Input Data for History-Matching Example Case 12.3.3 Permeability ratio data Absolute permeability (md) Zone thickness (ft) Zone 1 Zone 2 Zone 1 Zone 2 1 Originaldata 9.6 7.2 17.0 14.0 2 Firstiteration 9.6 7.2 17.0 14.0 3 Firstiteration 9.6 7.2 13.6 11.2 4 Firstiteration 7.7 5.7 17.0 14.0 5 Firstiteration 5.9 4.4 22.0 18.2 6 Seconditeration 5.9 4.4 22.0 18.2 Summary Comments Concerning History-Matching Example Nowthatamodelhasbeenobtainedthatmatchestheavailableproductiondataandcanbeusedto predictfutureoilandgasproductionrates,anassessmentofthemodificationstothedatathatwere performedduringthehistorymatchshouldbemade.Table12.8containsinformationconcerning thedatathatwerevariedinthesixcasesthathavebeendiscussed. Allotherinputdatawereheldconstantattheoriginalvaluesforallsixcases.Thefirstand second iterations of the gas-to-oil permeability ratio data led to values higher than the original data,ascanbeseeninFigure12.13.Inthelastsection,severalreasonsforadiscrepancybetween laboratory-measuredpermeabilityratiovaluesandfield-measuredvalueswerediscussed.These reasonsincludedgreaterdrawdowninareasclosertothewellborethaninareassomedistanceaway fromthewellbore,completionandplacingonproductionofsomewellsbeforeothers,twoormore strataofvaryingpermeabilities,andgravitydrainageeffects.Allthesephenomenaleadtounequal stagesofdepletionwithinthereservoir.Theunequalstagesofdepletioncausevaryingsaturations throughout the reservoir and hence varying effective permeabilities. The data plotted in Figure 12.13suggestthatthediscrepancybetweenthelaboratory-measuredpermeabilityratiovaluesand thefield-determinedvaluesisnotgreatandthattheuseofthemodifiedpermeabilityratiovalues inthematchingprocessisjustified. Forthefinalmatchincase6,thezonethicknesseswereincreasedbyabout30%overthe originaldataofcase1,andtheabsolutepermeabilitieswerereducedbyabout39%.Atfirstglance, thesemodificationsinzonethicknessandabsolutepermeabilitymightseemexcessive.However, remember that the values of zone thickness and absolute permeability were determined in the laboratoryonacoresample,approximately6in.indiameter.Althoughthetechniquesusedinthe laboratoryareveryaccurateintheactualmeasurementoftheseparameters,toperformthehistory match,itwasnecessarytoassumethatthemeasuredvalueswouldbeusedasaveragevaluesover theentire40-acdrainageareaofthewell.Thisisaverylargeextrapolation,andtherecouldbesignificanterrorinthisassumption.Ifthesmallmagnitudesoftheoriginalvaluesareconsidered,the adjustmentsmadeduringthehistory-matchingprocessarenotlargeinmagnitude.Theadjustments wereonly2.8mdto3.7mdand4.2ftto5.0ft.Thesenumbersarelargerelativetotheinitialvalues butarecertainlynotlargeinmagnitude. Chapter 12 466 • History Matching Itcanbeconcludedthatthemodeldevelopedtoperformthehistorymatchforthewellin questionisreasonableanddefendable.Moresophisticatedequationscouldhavebeendeveloped, butforthisparticularexample,theSchilthuismaterialbalancecoupledwithaflowequationwas quiteadequate.Aslongasthesimpleapproachmeetstheobjectives,thereisgreatmeritinkeeping thingssimple.However,thereadershouldrealizethattheprinciplesthathavebeendiscussedabout historymatchingareapplicablenomatterwhatdegreeofmodelsophisticationisused. Problems 12.1 Thefollowingdataaretakenfromavolumetric,undersaturatedreservoir.Calculatetherelativepermeabilityratiokg/koateachpressureandplotversustotalliquidsaturation: Connatewater,Sw=25% Initialoilinplace=150MMSTB Boi=1.552bbl/STB p (psia) R (SCF/STB) Np (MM STB) Bo (bbl/STB) Bg (bbl/SCF) Rso (SCF/STB) μo/μg 4000 903 3.75 1.500 0.000796 820 31.1 3500 1410 13.50 1.430 0.000857 660 37.1 3000 2230 20.70 1.385 0.000930 580 42.5 2500 3162 27.00 1.348 0.00115 520 50.8 2000 3620 32.30 1.310 0.00145 450 61.2 1500 3990 37.50 1.272 0.00216 380 77.3 12.2 Discusstheeffectofthefollowingontherelativepermeabilityratios,calculatedfromproductiondata: Errorinthecalculatedvalueofinitialoilinplace Errorinthevalueoftheconnatewater Effectofasmallbutunaccountedforwaterdrive Effectofgravitationalsegregation,bothwherethehighgas-oilratiowellsareshutin andwheretheyarenot (e) Unequalreservoirdepletion (f) Presenceofagascap (a) (b) (c) (d) 12.3 ForthedatathatfollowandaregiveninFigs.12.15to12.17andthefluidpropertydata presentedinthechapter,performahistorymatchontheproductiondatainFigs.12.18to 12.21,usingtheExcelworksheetinTable12.4.Usethenewpermeabilityratiodataplotted Problems 467 inFigs.12.8and12.13tofine-tunethematch.Thefollowingtableindicateslaboratorycore permeabilitymeasurements: Well Average absolute permeability to air (md) Zone 1 Zone 2 5-6 5.1 4.0 8-16 8.3 6.8 9-13 11.1 6.0 14-12 8.1 7.6 2 3 4 5 11 10 9 8 – 400 12 – 500 9-4 9-3 9-2 9-1 9-5 9-6 9-7 9-8 9-12 9-11 9-10 9-9 – 600 13 14 15 24 23 22 9-13 9-14 9-15 9-16 16 17 21 20 – 700 – 800 – 900 Figure 12.15 Structural map of well locations for Problem 12.3. 2 4 3 5 5' 10' 20' 11 15' 10 9 8 16 17 20' 10º 15 14 13 20' 15' 10' 24 23 22 21 20 4 5 10' Figure 12.16 Isopach map of zone 1 for Problem 12.3. 2 3 10' 11 10' 10 9 8 15' 10' 13 14 15 16 15' 17 15' 15' 24 23 22 21 15' Figure 12.17 Isopach map of zone 2 for Problem 12.3. 468 20 60 1200 Oil production GOR × × 40 800 × × 30 × 600 × 20 10 400 × 200 1 Figure 12.18 2 3 4 5 Time, years 6 7 8 Actual oil production and instantaneous GOR for well 5-6 for Problem 12.3. 60 1200 × Oil production GOR Oil rate, STB/day 50 1000 × 40 × 30 × × 1 Figure 12.19 800 600 × × 20 10 GOR, SCF/STB 1000 GOR, SCF/STB Oil rate, STB/day 50 400 × 200 2 3 4 5 Time, years 6 7 8 Actual oil production and instantaneous GOR for well 8-16 for Problem 12.3. 469 70 1200 60 1000 50 800 × 40 600 × 30 20 × GOR, SCF/STB Oil rate, STB/day × Oil production GOR 400 × 200 × 1 2 3 4 5 Time, years 6 7 8 Figure 12.20 Actual oil production and instantaneous GOR for well 9-13 for Problem 12.3. Oil rate, STB/day × 1200 Oil production GOR 50 1000 40 800 × 30 × 20 × 400 × × 10 600 GOR, SCF/STB 60 × × 1 2 200 3 4 5 Time, years 6 7 8 Figure 12.21 Actual oil production and instantaneous GOR for well 14-12 for Problem 12.3. 470 References 471 12.4 CreateanExcelworksheetthatusestheMuskatmethoddiscussedinChapter10inplace oftheSchilthuismethodusedinChapter12toperformthehistorymatchonthedatain Chapter12. 12.5 CreateanExcelworksheetthatusestheTarnermethoddiscussedinChapter10inplace oftheSchilthuismethodusedinChapter12toperformthehistorymatchonthedatain Chapter12. References 1. A.W.McCray,Petroleum Evaluations and Economic Decisions,PrenticeHall,1975. 2. H.B.Crichlow,Modern Reservoir Engineering—A Simulation Approach,PrenticeHall,1977. 3. P.H.YangandA.T.Watson,“AutomaticHistoryMatchingwithVariable-MetricMethods,” Society of Petroleum Engineering Reservoir Engineering Jour.(Aug.1988),995. 4. T.Ertekin,J.H.Abou-Kassem,andG.R.King,Basic Applied Reservoir Simulation,Vol.10, SocietyofPetroleumEngineers,2001. 5. J.Fanchi,Principles of Applied Reservoir Simulation,3rded.,Elsevier,2006. 6. C.C.MattaxandR.L.Dalton,Reservoir Simulation,Vol.13,SocietyofPetroleumEngineers, 1990. 7. M.Carlson,Practical Reservoir Simulation,PennWellPublishing,2006. 8. J.J.Arps,“AnalysisofDeclineCurves,”Trans. AlME(1945),160,228–47. 9. J.J.Arps,“EstimationofPrimaryOilReserves,”Trans. AlME(1956),207,182–91. 10. M. J. Fetkovich, “Decline CurveAnalysis Using Type Curves,” J. Pet. Tech. (June 1980), 1065–77. 11. R.G.Agarwal,D.C.Gardner,S.W.Kleinsteiber,andD.D.Fussell,“AnalyzingWellProductionDataUsingCombined-Type-CurveandDecline-CurveAnalysisConcepts,”SPE Res. Eval. & Eng. (1999),2,478–86. 12. T.Ahmed,Reservoir Engineering Handbook, 4thed.,GulfPublishingCo.,2010. 13. I.D.Gates,Basic Reservoir Engineering,KendallHuntPublishing,2011. 14. PersonalcontactwithD.W.Green. 15. T.D.Mueller,J.E.Warren,andW.J.West,“AnalysisofReservoirPerformanceKg/KoCurves andaLaboratoryKg/KoCurveMeasuredonaCoreSample,”Trans.AlME(1955),204,128. This page intentionally left blank Glossary Absolute permeability The permeability of a flow system that is completelysaturatedwithasinglefluid. Absolute pressure Pressuremeasuredrelativetoavacuum. Allowable A production rate limit set by a regulatory agency to maximize the overall recovery fromareservoir. Anticline Ageologicalstructurethatformsahydrocarbontrap.Itisafoldthatisconvexdown. API AnabbreviationfortheAmericanPetroleum Institute. API gravity Theweightofahydrocarbonliquidrelative toanequalvolumeofwater.Purewaterhas anAPIgravityof10.AhigherAPIgravity indicatesalessdenseliquid. Aquifer Asubsurfacegeologicformationconsisting ofinterstitialwaterstoredinporousrock. 473 Areal sweep efficiency Thefractionorpercentageoftheareaofthe reservoir swept by an injected fluid in the totalreservoirareaduringflooding. Artificial lift A system that adds energy to the fluid column in the wellbore to improve production.Artificialliftsystemsincluderod pumping,gaslift,andelectricsubmersible pump. Associated gas Thehydrocarbongasreleasedfromaliquid at the surface. Also referred to as solution gas or dissolved gas. Average reservoir pressure Avolumetricaverageofthepressureexerted byfluidsinsidethereservoir. Azimuth The angle that characterizes a direction or vectorrelativetoareferencedirection. Bitumen Hydrocarbonfluidwithagravityof10°API or lower. 474 Boundary conditions Thepropertiesorconditionsassignedtothe theoreticalboundariesusedinsolvingdifferentialequationslikethoseinwelltesting. Bounded reservoir Isolatedreservoirswithboundariesthatprohibitcommunication. Bubble point The pressure and temperature conditions at whichthefirstbubbleofgasevolvesfroma solution. Buildup test See pressure buildup test. Cap rock Impermeablerockthatformsabarrierabove and around the reservoir rock, preventing migrationfromandpromotingaccumulation inthereservoirrock. Carbonate rock A class of sedimentary rock composed of carbonatematerials. Casing The major structural component of a wellbore consisting of a steel pipe cemented in place. Casing prevents the formation wall from caving into the wellbore, isolates differentformations,andprovidesthepathway fortheproductionofwellfluids. Condensate Hydrocarbon liquid that is condensed from a gas phase as pressure and/or temperature changes; it typically has an API gravity greaterthan60°API. Glossary Connate water Watertrappedintheporesofarock. Core A cylindrical section of rock drilled from a reservoirsection.Acoreisusedtodetermine reservoirpropertieslikepermeability,porosity, and so on. Critical point The pressure and temperature conditions abovewhichthesubstancebecomesasupercriticalfluid—afluidinwhichthereisnodistinctionbetweenthegasandliquidphases. Darcy Aunitofrockpermeability. Darcy’s law Alawpredictingthefluidflowratethrougha porousmediumduetopressuredifferential. Dead oil Oilthathaslostitsvolatilecomponentsand containsnodissolvedgas. Displacement efficiency Theratioofthevolumeofoilinrockpores displacedbyaninjectedfluidtotheoriginal volume of oil at the beginning of the enhancedrecoveryprocess. Emulsion Amixtureofliquids,whereoneliquidisdispersed as droplets in the continuous phase createdbytheotherliquid. Enhanced oil recovery A generic term for techniques used to increase the amount of crude oil that can be extractedfromanoilfield. Glossary EOR Abbreviationforenhanced oil recovery. Fault A fracture or discontinuity in a geologic structure. Formation damage A reduction in permeability near the wellboreofareservoirformation. Fracturing Hydraulicfracturingisamethodoffracturingrockbymeansoftheinjectionofpressurized fluid into a reservoir through the wellbore. Gas formation volume factor Thisfactoristheratioofthegasvolumeat reservoir conditions and the gas volume at standardconditions. Gas-oil contact A transitional zone containing gas and oil, abovewhichtheformationcontainspredominatelygasandbelowwhichispredominately oil. Gas saturation Thefractionofporespaceoccupiedbygas. Gas-water contact Atransitionalzonecontaininggasandwater, abovewhichtheformationcontainspredominatelygasandbelowwhichispredominatelywater. History matching In reservoir simulation, history matching is anattempttobuildamodelthatwillmatch pastproductionfromawell. 475 Horner plot TheHornerplotisaplotofpressureversusa functionoftimeduringapressurebuilduptest. Hydrate Atermusedtoindicatethatasubstancecontainswater. Hydrocarbon Achemicalcompoundthatconsistsonlyof the elements hydrogen and carbon. Natural gasandoilarespeciesofhydrocarbon. Hydrocarbon trap A trap is a geologic structure that impedes the flow of hydrocarbons, resulting in a localizedaccumulationofhydrocarbons. Injection well A well that is used to inject fluid into the reservoirratherthanproducefluidfromthe reservoir. Isopach map Amapthatillustratesthevariationsinthicknessofageologiclayer. LNG Liquefied natural gas. Natural gas, mostly methane,convertedtoalow-temperaturefluid. LPG Liquefied petroleum gas.A mixture of primarilypropaneandbutane. Mass density Aratioofmasstovolume. Mobility Theratioofthepermeabilityovertheviscosityofareservoirfluid. 476 Glossary Natural gas Anaturallyoccurringhydrocarbongasmixtureconsistingprimarilyofmethane. Permeability Ameasureoftheabilityofaporousmaterial toallowfluidstopassthroughit. NGL Natural gas liquids. Components of natural gas that are separated from the gas state in theformofliquids. Petroleum Anaturallyoccurringflammableliquidconsistingofamixtureofvarioushydrocarbons. Nonconformity See unconformity. Phase Aphysicallydistinctiveform,suchassolid, liquid,andgasstatesofasubstance. Oil formation volume factor Theratioofthevolumeoftheoilatreservoir conditionstothevolumeoftheoilatstock- tankconditions. Porosity Alsocalledvoid fraction,itistheratioofthe volumeofthevoidspaceinamaterialtothe volumeofthematerial. Oil saturation Thefractionofporespaceoccupiedbyoil. Pressure buildup test An analysis of bottom-hole pressure data generatedwhenawellisshutinafteraperiodofflow.Thepressureprofileisusedto assess the extent and characteristics of the reservoirandthewellborearea. Oil-water contact Atransitionalzonecontainingoilandwater, abovewhichtheformationcontainspredominatelyoilandbelowwhichispredominately water. Oil-wet rock Reservoirrockthatmaintainscontactwitha layerofoil. OOIP Originaloilinplace.Totalinitialhydrocarboncontentofareservoir. Overburden Rockorsoiloverlyingareservoir. Paraffin Paraffinwaxisasoftsolidderivedfromhydrocarbonmolecules. Pressure transient test Ananalysisofbottom-holepressuredatagenerated while a limited amount of fluid is allowedtoflowfromthereservoir.Thepressure profileisusedtoassesstheextentandcharacteristicsofthereservoirandthewellborearea. Primary recovery The first stage of hydrocarbon production, characterizedbyproductionofhydrocarbons fromthereservoirusingonlythenaturalreservoir energy. Producing gas-oil ratio Theratioofthevolumeoftheproducedgas to the volume of the produced oil, both at standardconditions. Glossary 477 Production wells Wellsusedtoproducehydrocarbonfromthe reservoir. Seep Aslowflowofhydrocarbongasorliquidto theEarth’ssurface. Reserves Volumeofhydrocarbonthatcanbeeconomicallyrecoveredfromareservoirusingcurrenttechnology. Shale Asedimentaryrockcomposedofconsolidatedclayandsilt. Reservoir A subsurface geologic structure with sufficientporositytostorehydrocarbons. Reservoir rock Theporousrockstoringhydrocarbonsinthe reservoir. Residual oil Oilthatdoesnotmovewhenfluidsareflowingthroughtherock. Salt dome Amushroom-shapedintrusionofshaleinto overlyingcaprock. Sandstone Asedimentaryrockconsistingofconsolidated sand. SCF Standardcubicfeet.Acommonmeasurefor a volume of gas, the actual volume is convertedinstandardconditions,normally60°F and14.7psia. Secondary recovery The second stage of hydrocarbon production, characterized by production of hydrocarbonsfromthereservoirviainjectionofan externalfluidsuchaswaterorgas. Skin Azoneofreducedorenhancedpermeability aroundawellboreoftenasaresultofperforation,stimulation,ordrilling. Skin factor Adimensionlessfactorusedtodeterminethe production efficiency of a well. Positive skin indicatesimpairmentofwellproductivitywhile negativeskinindicatesenhancedproductivity. Solution gas Dissolvedgasinreservoirfluid. Solution gas-oil ratio The volumetric ratio of solution gas to the oilsolvent. Source rock Organic-rich rock, which, with heat and pressure,willgenerateoilandgas. Specific mass Themassperunitvolumeofasubstanceat referenceconditions. Specific weight Theweightperunitvolumeofasubstanceas referenceconditions. Standard pressure Areferencepressureusedtodetermineproperties,likespecificmassandspecificweight, 478 Glossary andstandardvolumes,suchasstandardcubicfeetorstock-tankbarrels. ofhydrocarbonthroughapermeablerockis haltedbyarelativelyimpermeablecaprock. Standard temperature A reference temperature used to determine properties, like specific mass and specific weight,andstandardvolumes,suchasstandardcubicfeetorstock-tankbarrels. Unconformity Asurfacebetweensuccessivegeologicstrata representingagapinthegeologicrecord. STB Stocktankbarrel.Acommonmeasurefora volumeofoil,theactualvolumeisconverted in standard conditions, normally 60°F and 14.7psia. Steady-state flow Aconceptusedinanalyzingsystemsthatassumes that all properties of the system are unchangingintime. Stock-tank conditions Standard conditions, normally defined as 60°Fand14.7psia. Sweep efficiency Inreservoirwaterfloodorgasflood,thefractionofreservoirareafromwhichthereservoirfluidisdisplacedbytheinjectedfluid. Syncline A trough-shaped rock fold that is convex down.Synclinesarenothydrocarbontraps. Tertiary recovery A stage of hydrocarbon production that is characterizedbyproductionofhydrocarbons fromthereservoirviainjectionofanexternalfluidsuchaswater,steam,orgas. Traps Anaccumulationofhydrocarboninaformationthatoccurswhentheupwardmigration Unitization Theconsolidationoftheindividualprivate mineralrightsofapetroleumreservoir.The unitization allows the unitized block to be developedmoreefficientlythaniftheindividualmineralownersactedindependently. Viscous fingering A condition in which an interface between twofluidshasanunevenorfingeredprofile, typicallycausedbyinconsistentrockpermeability.Viscousfingeringtypicallyresultsin lowsweepefficienciesinwaterflooding. Water saturation Thefractionofporespaceoccupiedbywater. Water-wet rock Reservoirrockthatmaintainscontactwitha layerofwater. Weight density Weightperunitvolumeofasubstance. Wellhead Asystemofpipe,valves,andfitting,locatedatthetopofthewellbore,thatprovides pressure and flow control of a production well. Well log The measurement versus depth of one or morephysicalquantitiesinawell. Glossary Wettability Thepreferenceoftherockformationtocontactonephaseoveranother. 479 Wildcat well Anexploratorywelldrilledinlandnotknown tobeanoilfield. This page intentionally left blank Index A AAPG.SeeAmericanAssociationof PetroleumGeologists Abou-Kassem.SeeDranchuk AGA.SeeAmericanGasAssociation Agarwal,Al-Hussainy,andRamey,97 Al-HussainyandRamey,261 Al-Hussainy,Ramey,andCrawford,240–41 Alkalineflooding,412,421,424–25 AllardandChen,323–24 Allen,121 AllenandRoe,143–45 Allowableproductionrate,473 AmericanAssociationofPetroleumGeologists (AAPG),2 AmericanGasAssociation(AGA),2 AmericanPetroleumInstitute(API),2 AmericanSocietyforTestingandMaterials (ASTM),24 AnschutzRanchEastUnit,152 Anticline,473 API.SeeAmericanPetroleumInstitute Aquifers,6 ArcaroandBassiouni,97–98 Arealsweepefficiency,366–67,473 Arps,164–65,438 Artificiallift,219,250,473 Ashman.See Jogi Associatedgas,2,28,67,80,473 ASTM.SeeAmericanSocietyforTestingand Materials “Attic”(updip)oil,382 481 Azimuth,473 Aziz.SeeMattar B BaconLimeZone,143 Barnes. SeeFancher Bassiouni.SeeArcaro Beddingplanes,163–64,229–30. See also Undersaturatedoilreservoirs bottomwaterdrive,163–64 edgewaterdrive,163–64 inmeasuringpermeability,229–30 BeggsandRobinson,55–56 Bellgasfield,28,33,35,89,92–96 Berry. SeeJacoby Bierwangfield,97 BigSandyreservoir,45,47–49,68 Bitumen,473 Blackoil,12,53 Blackwell.SeeRichardson Blasingame,38–40 Bobrowski.See Cook Borshcel.SeeSinha Botset.SeeWycoff Bottom-holepressure,4,67–68,265–66,289– 90,476 Bottom-holepressuregauge,4 Boundaryconditions,264,305,474 Boundedreservoir,474 Bourgoyne,Hawkins,Lavaquial,and Wickenhauser,110 Boyd. SeeMcCarthy 482 Boyle’slaw,22,24 Brady. SeeLutes Brar. SeeMattar Bruskotter.SeeRussel Bubblepoint,474 Bubble-pointpressure,5,11,45–47,50–56, 210–11,221–24 Buckley.See Craze;Tarner BuckleyandLeverett,6,369–75.See also Displacement,oilandgas Builduptesting,277–82 Hornerplot,279–82,475 pseudosteady-statetimeregionin,277–78 shut-inpressure,279–80 skinfactorin,274–77 superposition,useof,267–72 Burrows.See Carr C Calculation(initial),gasandoil,124–31 Callaway. SeeSteward Calvin. SeeKleinsteiber CanyonReefreservoir(Kelly-Snyderfield, Texas),171–76,384 Capillarynumber,412–14,421,424 Capillarypressure,24,220,357–58 Caprock,474,477–78 Carbonaterock,474 Carpenter,Schroeder,andCook,210 Carr,Kobayashi,andBurrows,41–42 CarterandTracy,323,346 Casing,474 Caudle.SeeSlobod Charles’slaw,24 Chatas,322 Chemicalfloodingprocesses,421–26.See also Tertiaryoilrecovery alkalineprocesses,424–25 micellar-polymerprocesses,422–24 microbialflooding,425–26 polymerprocesses,421–22 problemsinapplying,426 Index Chen.See Allen Chiang.SeeLutes Chin.See Cook Christensen,411 ClarkandWessely,6 Coats,323 Coleman,Wilde,andMoore,5 Compressibilityfactors,21,30,36,192, 196,222–24.See alsoGasdeviation factor;Isothermalcompressibility; Supercompressibilityfactor Condensate,474 Connatewater,5,149,194–97,283–84,474 ConroeField(Texas),203–8,220,299–301, 350–51 Contingentresources,3–4 Cook. SeeCarpenter Cook,Spencer,andBobrowski,217 Cook,Spencer,Bobrowski,andChin,161 Core,474 CoreLaboratoriesInc.,160,211–15 Crawford.SeeAl-Hussainy CrazeandBuckley,163 Cricondentherm,9–10,131 Criticalpoint,9,415,418–19,474 Criticalsaturation,360–61,400–401,423 Crudeoilproperties,44–60 correlations,44 formationvolumefactor(Bo)47–51 isothermalcompressibility,51–53 saturatedvs.undersaturated,44 solutiongas-oilratio(Rso),21,44–47,61– 62,477 viscosity,53–60 D Darcy,5 Darcy,asunitofmeasure,474 millidarcy,228–29,249–50 Darcyflow,347 Darcy’slaw,227–32,236–39,245,247–48, 297,474 Index Davis.SeeFatt DDI.SeeDepletiondriveindex Deadoil,55,121,474 Depletiondriveindex(DDI),80–81,204–6, 217,220 Dew-pointpressure,9,27–28,122–23,141– 42,152 Differentialprocess,145–47,209–10,214 Displacementefficiency,357–59,365–69,474 Displacement,oilandgas,357–404 Buckley-Leverettdisplacementmechanism, 369–75 enhancedoilrecoveryprocesses(EOR) alkalineflooding,412,421,424–25 capillarynumber,412–14,421,424 chemicalfloodingprocesses,421–26 dynamicmiscibleprocess,417–19 forwarddrycombustionprocess,430 forwardwetcombustionprocess,430 insitucombustion,430 misciblefloodingprocesses,414–21 multiple-contactmiscibleprocess,417–20 inoil-wetsystems,42 polymerflooding,421 residualoil,mobilizationof,412–14 single-contactmiscibleprocess,415–17 steam-cyclingorstimulationprocess,428 steam-driveprocess,428–30 thermalprocesses,427–31 inwater-wetsystems,412 immiscibleprocesses,369–99 macroscopicdisplacementefficiency,365–69 anisotropyofhydro-carbon-bearing formation,effecton,365–66 arealsweepefficiency,366–67,473 heterogeneitiesofhydro-carbon-bearing formation,365–66 limestoneformations,366,369 pressuremaintenance,152–53,172,176, 222 sandstoneformations,369 483 viscousfingering,366,406–7,411,414, 421–26,478 mechanism dragzone,375 floodfront,244,284,361,366,375, 401–2 oilbank,375,414,423,433 microscopicdisplacementefficiency,357– 59 absolutepermeability,359–60,399–402 capillarypressure,24,220,357–58 criticalsaturation,360–61,400–401,423 fractionalflowcurve,364–65,377 hydrocarbonsaturation,150,361 interfacialtensionsbetweenfluids,358, 362 relativepermeability,359–65 residualsaturation,361–62,417–18 transitionzone,362–264,371–74,381, 400–401 wettability,357–58,424,479 oilrecoverybyinternalgasdrive,382–99 iterationtechniques,390 secantmethod,390 recoveryefficiency,357–69 relativepermeability,359–65 waterflooding,14,233,405–6,412,422, 478 direct-line-drive,367,408 patternflooding,407 peripheralflooding,407,409 Displacement,oilbygas downdipoil,377–78,382 gravitationalsegregationin,376–82 oilrecoverybyinternalgasdrive,382–99 oil-wetrock,475 updip(“attic”)oil,382 waterwetrock,478 Dissolvedgas,2 Distillate,121 Dotson,Slobod,McCreery,andSpurlock,22 484 Downdipoil,377,78,382 Downdipwaterwells,97 DranchukandAbou-Kassem,31,38 Drawdowntesting,272–74 Drygas,66,103,117,153–56,416–20.See alsoLeangas E Eakin. SeeLee Earlougher,262,267 Earlougher,Matthews,Russell,andLee,272 EastTexasfield,82 EchoLakefield,113 Economics,inrelationtogas,18 Egbogah,55 Eilerts,32.See alsoMuskat ElkBasinfield(WyomingandMontana),161 ElkCityfield(Oklahoma),217 Ellenburgerformation(WestTexas),296 Emulsion,474 Enhancedoilrecovery(EOR),14,405–35,474 introductionto,405–6 secondary,406–12.See alsoSecondaryoil recovery tertiary,412–33.See alsoTertiaryoil recovery EOR. SeeEnhancedoilrecovery Equationsofstate,24.See alsoIdealgaslaw; Pressure-volume-temperature Equilibriumratios,138–40,144–47 Estimatedultimaterecovery(EUR),4 EUR. SeeEstimatedultimaterecovery Excel,439,448–55,466,471 Ezekwe,22,24,44 F Fancher,Lewis,andBarnes,5 Farshad.SeeRamagost FattandDavis,237 Fault,475 Fetkovich,6,346–50,355,438 Index Flashprocess,145,209–10,214.See also Saturatedoilreservoirs Floodfront,244,284,361,366,375,401–2 Fluidflow,single-phase.SeeSingle-phasefluid flow Fluidsaturations,24 Formationdamage,475 Formationvolumefactor(Bo),34–35,47–51,61 Fracking.SeeFracturing Fractionalflowcurve,364–65,377 Fracturing,4,17–18,250,407–9,475 Freegasvolume,49,75,77,83 G Gasandoil(initial)calculation,124–31 Gascompressibilityfactor,21,36,223 Gas-condensatereservoirs,121–58 calculatinginitialgasandoilin,124–31 leangascyclingandwaterdrivein,147–51 performanceofvolumetricreservoirs,131–40 predictedvs.actualproductionhistoriesof volumetricreservoirs,143–47 useofmaterialbalancein,140–43 useofnitrogenforpressuremaintenancein, 152–53 Gasdeviationfactor,27–37,100–17,125–27, 141–42,153–55 Gasdistillate,2 Gasformationvolumefactor,34,76,239,444, 475 Gas-oilcontact,475 Gas-oilratio(GOR),21,44–47,61–62,477 asacrudeoilproperty,44–47 historymatchingand,453 netcumulativeproducedinvolumetric,169 solutionGORinsaturatedoilreservoirs, 215–17 Gasproperties,24–43 formationvolumefactoranddensity,34–35 gasdeviationfactor,27–37,100–17,125– 27,141–42,153–55 Index idealgaslaw,24–25 isothermalcompressibility,35–41 realgaslaw,26–34 specificgravity,25–26 supercompressibilityfactor,26–27 viscosity,41–43 Gasreservoirs.See alsoGas-condensate reservoirs;Single-phasegasreservoirs abnormallypressured,110–12 asstoragereservoirs,107–9 Gassaturation,475 Gasvolumefactors,35,65,89–93,112–14 Gas-watercontact,7,114,475 Geertsma,23–24 Geffen,Parish,Haynes,andMorse,95 Generalmaterialbalanceequation.See Materialbalanceequation Gladfelter.SeeStewart GlenRoseFormation,143 Gloyd-MitchellZone(Rodessafield),177–84 averagemonthlyproductiondata,179–80 development,production,andreservoir pressurecurves,177 gasexpansion,177,181 liquidexpansion,177,181 productionhistoryvs.cumulativeproduced oil,181 productionhistoryvs.time,181 solutiongas-drivereservoir,171 Gonzalez.SeeLee Goodrich.SeeRussel GOR.SeeGas-oilratio Gravitationalsegregationcharacteristics,219– 220,402,453 displacementofoilbygasand,376–82 Gray.See Jogi H Hall,184 Harrison.See Rodgers HarvilleandHawkins,110 485 HavlenaandOdeh,73,83–85.See also Materialbalanceequation Hawkins.SeeBourgoyne,Harville Haynes.SeeGeffen Hinds.SeeReudelhuber Historymatching,437–71,475 declinecurveanalysis,437–41 developmentofmodel,441–42 incorporatingflowequation,442 materialpartofmodel,441 exampleproblem,449–46 discussionofhistory-matchingresults, 451–65 fluidpropertydata,conversionof,448– 49,451–53 solutionprocedure,449–51 summarycommentsconcerning,465–66 gas-oilratios,453 gasproductionrate,465 multidimensional,multiflowreservoir simulators,437 oilproductionrate,451 zero-dimensionalSchilthuismaterial balanceequation,441–42 HoldenField,116 Holland.SeeSinha Hollis,109 Horizontaldrilling,17–18,434 Hornerplot,279–82,475 Hubbert,15 Hubbertcurve,15–16 Hurst,6,274,303–6,322–23,349–50 Hydrate,475 Hydraulicfracturing,4,17–18,250,407–9,475 Hydraulicgradients,228,230 Hydrocarbonsaturation,150,361 Hydrocarbontrap,475 I Idealgaslaw,24–25 IEA.SeeInternationalEnergyAgency 486 Index Ikoku,108 Initialunitreserve,92–93 Injectionwells,475 InternationalEnergyAgency(IEA),16 Interstitialwater,83,92,115,162,473 Ira Rinehart’s Yearbooks,121–23 Isobaricmaps,82 Isopachmaps,82,88,102,455,468,475 Isothermalcompressibility,21–24,76,233,260 ofcrudeoil,51–53 ofgas,35–41 ofreservoirwater,62–63 Leverett.SeeBuckley LeverettandLewis,5 Lewis.SeeFancher;Leverett Limestoneformations,23 Linearflow,233,236–37,242–45,254,371 Liquefiednaturalgas(LNG),475 Liquefiedpetroleumgas(LPG),135,415,475 LNG.SeeLiquefiednaturalgas LouisianaGulfCoastEugeneIslandBlock Reservoir,98 LPG.SeeLiquefiedpetroleumgas Lutes,Chiang,Brady,andRossen,97 J Jackson.SeeMatthes JacobyandBerry,217 Jacoby,Koeller,andBerry,140 Jogi,Gray,Ashman,andThompson,110 Jonessand,89–90 M Marudiak.SeeMatthes Massdensity,475 Materialbalanceequation,73–85 calculatinggasinplaceusing,98–105 derivationof,73–81 driveindicesin,202–6 ingas-condensatereservoirs,140–43 HavlenaandOdehmethodofapplying, 83–85 historymatchingwith,441 insaturatedoilreservoirs,200–206 asastraightline,206–9 inundersaturatedoilreservoirs,167–71 usesandlimitationsof,81–83 volumetricgasreservoirs,98–100 water-drivegasreservoirs,100–105 zero-dimensionalSchilthuis,441–42 Mathews,Roland,andKatz,128 Mattar,Brar,andAziz,38–39 Matthes,Jackson,Schuler,andMarudiak,97 Matthews.SeeEarlougher MatthewsandRussell,254 Maximumefficientrate(MER),199,218–20 McCain,52,61–64,70 McCain,Spivey,andLenn,44,50 McCarthy,Boyd,andReid,107 McCord,161 K Katz.SeeMathews,Standing KatzandTek,107–8 Kaveler,90 Keller,Tracy,andRoe,218 Kelly-SnyderField(CanyonReefReservoir), 171–76,384 Kennedy.SeeWieland KennedyandReudelhuber,161 Kern,382 Kleinsteiber,Wendschlag,andCalvin,152–53 Kobayashi.See Carr Koeller.SeeJacoby L Laminarflow,228,244,253,274 LaSalleOilField,67 Lavaquail.SeeBourgoyne Leangas,140,147,152.See alsoDrygas Lee.SeeEarlogher Lee,Gonzalez,andEakin,43 Index McMahon.See van Evenlingen MEOR.SeeMicrobialenhancedoilrecovery MER.SeeMaximumefficientrate Mercury,132 Micellar-polymerflooding,421 Microbialenhancedoilrecovery(MEOR),425 MileSixPool(Peru),219,378–83 Millidarcy,228–29,249–50 MillikanandSidwell,4–5 Misciblefloodingprocesses,414–21.See also Tertiaryoilrecovery inertgasinjectionprocesses,420–21 multiple-contact,417–20 problemsinapplying,421 single-contact,415–17 Mobility,365–68,383–84,421–26,475 Moore.SeeColeman MooreandTruby,296 Morse.SeeGeffen Moscrip.SeeWoody Msand,114 Mueller,Warren,andWest,453 Muskat,198,384–85,393,397,402,471 Muskat,Standing,Thornton,andEilerts,121 N NationalInstituteforPetroleumandEnergy Research(NIPER),425 Naturalgasliquids,476 Netisopachousmap.See Isopachmaps Newman,23–24 NIPER.SeeNationalInstituteforPetroleum andEnergyResearch Nitrogen,forpressuremaintenance,152–53 Nonconformity.SeeUnconformity NorthSeagasfield.SeeRoughgasfield O OdehandHavlena,73,83–85 Oil and Gas Journal, The,172,425,434 Oilbank,375,414,423,433 487 Oilformationvolumefactor,51,76,80,196, 203,215,390,476 Oilsaturation,476 Oil-watercontact,7,297,305,320,353,362, 476 Oil-wetrock,476 Oilzone,2,11–13,74 Originaloilinplace(OOIP),196,224,476 Osif,62 Overburden,21,23,237,428,430,476 P Paradoxlimestoneformation,146 Paraffin,32,476 Parish.SeeGeffen Peakoil,14–18 Peoriafield,350,352 Permeability,476 absolute,359–60,399–402 beddingplanesand,229–30 recoveryefficiencyand,359–65 Perry.SeeRussell Petroleum,476 Petroleumreservoirs,1–4 productionfrom,13–14 typesbyphasediagrams,9–13 PetroleumResourcesManagementSystem (PRMS),2–3 Petrophysics,5 PI.SeeProductivityindex Pirson,80–81 Poiseuille’slaw,245 Porevolumecompressibility,21,23 Porosity,7,21–23,112–17,476 PR.SeeProductivityratio Pressure abnormal,110–12 absolute,24,473 average,66,75–76,80–82,140–41,441–42 bottom-hole,4,67–68,265–66,289–90, 476 488 Pressure(continued) bubble-point,5,11,45–47,50–56,210–11, 221–24,283,288,382 capillary,24,220,357–58 constantterminalpressurecase,304 dewpoint,9,27–28,122–23,141–42,152 standard,477 Pressurebuilduptest,278–79,291,475,476 Pressuremaintenanceprogram,152–53,172, 176,222 Pressuretransienttesting,272–82,476 builduptesting,277–82 Hornerplot,279–82,475 pseudosteady-statetimeregionin,277–78 shut-inpressure,279–80 skinfactorin,274–77 superposition,useof,267–72 drawdowntesting,272–74 Pressure-volume-temperature(PVT),5,154– 57,167–70,193–95,198,209–22,301 Primaryproduction,13,159,405–6,476 PRMS.SeePetroleumResourcesManagement System Production,3 primaryproduction(hydrocarbons),13, 159,405–6,476 secondaryrecoveryoperation.See Secondaryoilrecovery tertiaryrecoveryprocesses.SeeTertiaryoil recovery Productionwells,14,97,114,171,365–67, 407–8,477 Productivityindex(PI),254–66 injectivityindex,266 Productivityratio(PR),266–67 Properties,21.See alsoCrudeoilproperties; Gasproperties;Reservoirwaterproperties; Rockproperties Prospectiveresources,3 Psandreservoir,116 Pseudosteady-stateflow,261–64 Index drawdowntestingof,273–74 radialflow,261–64 compressiblefluids,264 slightlycompressiblefluids,261–64 waterinflux,346–50 PVT.SeePressure-volume-temperature Q Quantitiesofgasliberated,5 R Radialflow,233,236,246,250,254–55 RamagostandFarshad,110 Ramey.SeeAgarwal,Al-Hussainy, Wattenbarger RangelyField,Colorado,161 Realgaslaw,26–34 Recoverablegrossgas,140–41 Recoveryefficiency,357–69 macroscopicdisplacementefficiency,365–69 microscopicdisplacementefficiency,357–59 permeabilityand,359–65 waterfloodingand,409–11 Redlich-Kwongequationofstate,152 Reed. SeeWycoff Regier. See Rodgers Regressionanalysis,29,207 Reid. SeeMcCarthy Reserves,3,92–93,477 Reservoir engineering, 6 historyof,4–6 terminology,xix-xxv,7–8,473–79 Reservoirmathematicalmodeling,6 Reservoirpressure,5 Reservoirrock,477 Reservoirs bounded,474 combinationdrive,74,477 flowsystems latetransient,233–35,254 pseudosteady.SeePseudosteady-stateflow Index steady-state.SeeSteady-stateflowsystems transient.SeeTransientflow storage,107–9 Reservoirsimulation,6 Reservoirtypesdefined,9–13 Reservoirvoidagerate,219 Reservoirwaterproperties,61–64 formationvolumefactor,61 isothermalcompressibility,62–63 solutiongas-waterratio,61–62 viscosity,63 Residualgassaturation,95–96 Residualoil,477 Residualsaturation,361–62,417–18 Resource(hydrocarbons),2–3 Retrogradecondensation,9–10,141,147–48, 152 Retrogradeliquid,10–11,36–37,132 Reudelhuber.SeeKennedy ReudelhuberandHinds,217 RichardsonandBlackwell,376 Robinson.See Beggs Rockcollapsetheory,110 Rockproperties,21–24 fluidsaturation,24 isothermalcompressibility,22–24 porosity,22 Rodessafield.SeeGloyd-MitchellZone (Rodessafield) Rodgers,Harrison,andRegier,139–40,146 Roe. See Allen Roland. SeeMathews Rossen. SeeLutes RoughGasField,109 Rsandreservoir,193,198 Russell.SeeEarlougher;Matthews Russell,Goodrich,Perry,andBruskotter,240 S Sabinegasfield,65,115 Saltdome,477 489 SanJuanCounty,Utah,146 Saturatedoilreservoirs,199–225 differentialvaporizationandseparatortests, 215–17 factorsaffectingoverallrecovery,199–200 continuousuniformformations,200 gravitationalsegregationcharacteristics, 200 largegascaps,200 formationvolumefactorand,215–17 gasliberationtechniques,209–15 introductionto,199–200 materialbalanceasstraightline,206–9 materialbalancecalculationsfor,202–6 materialbalancein,200–209 maximumefficientrate(MER)in,218–20 solutiongas-oilratio,215–17 volatile,217–18 waterdrive bottomwaterdrive,323–46 edgewaterdrive,303–23 Saturation critical,360–61,400–401,423 gas,475 residual,361–62,417–18 residualhydrocarbon,150,361 Saturationpressure.SeeBubble-pointpressure Schatz.SeeSinha Schilthuis,5–6,302–3,441–52 Schroeder.SeeCarpenter Schuler.SeeMatthes Schulerfield,89 SclaterandStephenson,4 ScurryReefField,Texas,161,213 SDI.SeeSegregation(gascap)index SEC. SeeSecuritiesandExchange Commissions Secondaryoilrecovery gasflooding,411–12 waterflooding,406–11 candidates,407 490 Secondaryoilrecovery(continued) estimatingrecoveryefficiency,409–11 locationofinjectorsandproducers, 407–9 Secondaryrecoveryprocess,14,477.See also Secondaryoilrecovery SecuritiesandExchangeCommissions(SEC),2 Seep,477 Segregation(gascap)index(SDI),80–81, 204–5 Separatorsystems,8,218 Shale,477 ShreveandWelch,382 Shrinkagefactor,47 Shrinkageofoil,5 Simpson’srule,241 Single-phasefluidflow,227–93 builduptesting,277–82 classificationofflowsystems,232–367 Darcy’slawandpermeabilityin,227–32 drawdowntesting,272–74 pressuretransienttesting,272–82 productivityindex(PI),254–66 productivityratio(PR),266–67 pseudosteady-stateflow,261–64.See also Pseudosteady-stateflow radialdiffusivityequationand,251–53 skinfactor,274–77 steady-state,236–51.See alsoSteady-state flow superposition,267–72 transientflow,253–61.See alsoTransient flow Single-phasegasreservoirs,87–119 abnormallypressured,110–12 calculatinggasinplace usingmaterialbalance,98–105 involumetricgasreservoirs,98–100 inwater-drivegasreservoirs,100–105 calculatinghydrocarboninplace,88–98 unitrecoveryfromgasreservoirsunder Index waterdrive,93–98 unitrecoveryfromvolumetricgas reservoirs,91–93 gasequivalentofproducedcondensateand water,105–7 limitationsofequationsanderrors,112–13 asstoragereservoirs,107–9 Sinha,Holland,Borshcel,andSchatz,110 Skinfactor,274–77,280,477 Slaughterfield,82 SlobodandCaudle,7,368 Slurries,4 Smith,R.H.,383 SocietyofPetroleumEngineers(SPE),2 SocietyofPetroleumEvaluationEngineers (SPEE),2 Solutiongas-oilratio(Rso),21,44–47,61–62, 477 Sourcerock,477 SPE.SeeSocietyofPetroleumEngineers Specificgravity,25–26,127–28 Specificmass,477–78 Specificweight,477 SPEE.SeeSocietyofPetroleumEvaluation Engineers Spencer.See Cook Sphericalflow,227,233 Standardpressure,477 Standardtemperature,101,478 Standing.SeeMuskat StandingandKatz,28,30–31,34 STB. SeeStock-tankbarrel Steady-stateflow,236–51 capillariesandfractures,244–46 crossflow,244,289 definitionof,478 linearflow,478 ofcompressiblefluids,238–41 ofincompressiblefluids,236–37 permeabilityaveragingin,241–44 ofslightlycompressiblefluids,237–38 Index parallelflow,243–45 radialflow ofcompressiblefluids,247 ofincompressiblefluid,246–47 permeabilityaveragesfor,248–51 ofslightlycompressiblefluids,247 radii external,247 wellbore,247 viscousflow,244–45 waterinfluxmodels,297–302 Stephenson.SeeSclater Stewart,Callaway,andGladfelter,297 St.JohnOilfield,115 Stock-tankbarrel(STB),8,478 Stock-tankconditions,50,478 Stratigraphictraps,1–2 Subsurfacecontourmaps,88 SummitCounty,Utah,152 Supercompressibilityfactor,26–27.See also Gasdeviationfactor Superposition,267–72 Sutton,28,29,70 Sweepefficiency,14,147,154,165,357,366, 369,406,421–24,433,478 Syncline,478 T Tarner,384,390,393,397,399,402,471 TarnerandBuckley,6 Tek. SeeKatz Tertiaryoilrecovery,412–33 alkalineprocesses,424–25 chemicalfloodingprocesses,421–26 definitionof,478 micellar-polymerprocesses,422–24 microbialflooding,425–26 misciblefloodingprocesses,414–21 inertgasinjectionprocesses,420–21 multiple-contact,417–20 problemsinapplying,421 491 single-contact,415–17 mobilizationofresidualoil,412–14 polymerprocesses,421–22 problemsinapplying,426 processes,14 thermalprocesses,427–31 insitucombustion,430 problemsinapplying,430–31 screeningcriteriafor,431–33 steam-cyclingorstimulationprocess, 428 steam-driveprocess,428–30 Testing builduptesting,277–82 drawdowntesting,272–74 pressuretransienttesting,272–82 Thermalprocesses,427–31.See also Tertiary oilrecovery insitucombustion,430 problemsinapplying,430–31 screeningcriteriafor,431–33 steam-cyclingorstimulationprocess,428 steam-driveprocess,428–30 Thompson.See Jogi Thornton.SeeMuskat Timmerman.See van Everdingen TorchlightTensleepreservoir,297 Totalflowcapacity,249 Tracy,390–91.See alsoCarter;Kelly Transientflow,253–61 linesourcesolution,255 radialflow,compressiblefluids,260–61 radialflow,slightlycompressiblefluids, 253–59 Transitionzone,362–264,371–74,381,400– 401 Traps,1–2,478 hydrocarbon,475 stratigraphic,1–2 Trube,38 Truby.SeeMoore 492 U Unconformity,476–78 Undersaturatedoilreservoirs,159–98.See also Volumetricreservoirs calculatingoilinplaceandoilrecoveriesin, 162–67 fluids,159–61 formationandwatercompressibilitiesin, 184–91 Gloyd-MitchellZoneoftheRodessaField, 177–84 Kelly-SnyderField,CanyonReefReservoir, 171–76 materialbalancein,167–71 Unitization,478 UniversityofKansas,443 Unsteady-stateflow,6,302–46.See alsoWater influx bottomwaterdrive,323–46 constantterminalpressurecase,304 constantterminalratecase,303 edgewaterdrivemodel,303–23 Updip(“attic”)oil,382 USDepartmentofEnergy,433 V ValkoandMcCain,46 vanderKnaap,23 vanEverdingenandHurst,303–23.See also Waterinflux vanEverdingen,Timmerman,andMcMahon, 83 Vaporization,9–10,107,159,209–10 Velarde,Blasingame,andMcCain,46 Villena-Lanzi,53 Viscosity,475 ofcrudeoil,53–60 ofgas,41–43 ofreservoirwater,63 Viscousfingering,366,406–7,411,414,421– 26,478 Index Voidfraction.SeePorosity Volatileoilreservoirs,217–18.See also Saturatedoilreservoirs Volumetricmethod(forcalculatinggasin place),112,220 Volumetricreservoirs artificialgascap,169 beddingplanes bottomwaterdrive,323–46 edgewaterdrive,303–23 bubble-pointpressure,5,11,45–47,50–56, 210–11,221–24 calculatinggasinplacein,98–100 calculationofdepletionperformance,135– 40,148,150–54 calculationofinitialoilinplace materialbalancestudies,162 volumetricmethod,112,220 calculationofunitrecoveryfrom,91–93 effectivefluidcompressibility,185–86 freegasphase,11,45,169,173,190,199 hydrauliccontrol,163–64,200 materialbalancein,98–100,167–71 netcumulativeproducedgas-oilratio,169 performanceof,131–40 predictedvs.actualproductionhistoriesof, 143–47 underwaterdrive,6,93,164 Volumetricwithdrawalrate,298 W WAG.SeeWateralternatinggasinjection process Warren.SeeMueller Wateralternatinggasinjectionprocess(WAG), 411 Water-driveindex(WDI),80–81,204,205, 206 Water-drivereservoirs,95,100–105,376 Waterflooding,14,233,405–6,412,422,478 Waterinflux,295–356 Index constant,298,300,302,303,306,350,352 introductionto,295–97 pseudosteady-state,346–50 steady-state,297–302 reservoirvoidagerate,300–301 volumetricwithdrawalrate,298 waterinfluxconstant,300–301 unsteady-state,302–46 bottomwaterdrive,323–46 constantterminalpressurecase,304 constantterminalratecase,303 edgewaterdrivemodel,303–23 Watervolume,8 Water-wetrock,478 WattenbargerandRamey,239 WDI.SeeWater-driveindex Weightdensity,478 Welch.SeeShreve Welge,376,378,381 Wellhead,4,12,95,112,114,138,213,449, 478 Welllog,22,478 Wendschlag.SeeKleinsteiber 493 Wessely.See Clark West.SeeMueller WesternOverthrustBelt,152 Wetgas,12,27,144,147,152–57 Wettability,357–58,424,479 WichertandAziz,34 Wickenhauser.SeeBourgoyne WielandandKennedy,82 Wildcatreservoir,197 Wildcatwell,479 Wilde.SeeColeman WoodyandMoscrip,74 WorldPetroleumCouncil(WPC),2 WPC.SeeWorldPetroleumCouncil WycoffandBostet,5 Wycoff,Botset,andMuskat,367 Wycoff,Botset,Muskat,andReed,5 Y Yarborough.See Vogel Z z-factor,31,34,43 This page intentionally left blank THIS PRODUCT informit.com/register Register the Addison-Wesley, Exam Cram, Prentice Hall, Que, and Sams products you own to unlock great benefits. 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