PV Elite® 2019
Project Data Page:
PV Elite® 2019
Table of Contents
Cover Page
Title Page
Warnings and Errors:
Input Echo:
XY Coordinate Calculations:
Internal Pressure Calculations:
External Pressure Calculations:
Element and Detail Weights:
Wind Load Calculation:
Earthquake Load Calculation:
Center of Gravity Calculation:
Horizontal Vessel Analysis (Ope.)
MDMT Summary:
Vessel Design Summary:
1
2
3
4
7
8
10
11
12
13
15
16
28
29
Cover Page
PV Elite® 2019
DESIGN CALCULATION
In Accordance with ASME Section VIII Division 1
ASME Code Version
: 2017
Analysis Performed by : SPLM Licensed User
Job File
: C:\USERS\MOON\DESKTOP\SADDLE DESIGN.Pvdb
Date of Analysis
: Oct 21,2019
PV Elite 2019, January 2019
4:33pm
Title Page
PV Elite® 2019
Note:
PV Elite performs all calculations internally in Imperial Units
to remain compliant with the ASME Code and any built in assumptions
in the ASME Code formulas. The finalized results are reflected to show
the user's set of selected units.
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Warnings and Errors:
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Oct 21,2019
Class From To : Basic Element Checks.
==========================================================================
Class From To: Check of Additional Element Data
==========================================================================
There were no geometry errors or warnings.
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PV Elite Vessel Analysis Program: Input Data
Design Internal Pressure (for Hydrotest)
Design Internal Temperature
Type of Hydrotest
Hydrotest Position
Projection of Nozzle from Vessel Top
Projection of Nozzle from Vessel Bottom
Minimum Design Metal Temperature
Type of Construction
Special Service
Degree of Radiography
Use Higher Longitudinal Stresses (Flag)
Select t for Internal Pressure (Flag)
Select t for External Pressure (Flag)
Select t for Axial Stress (Flag)
Select Location for Stiff. Rings (Flag)
Consider Vortex Shedding
Perform a Corroded Hydrotest
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Load
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
Case
1
2
3
4
5
6
7
8
9
10
11
12
13
14
15
16
17
18
19
Wind Design Code
UBC Design Wind Speed
UBC Exposure Constant
UBC Importance Factor
UBC Base Elevation
UBC Percent Wind for Hydrotest
Using User defined Wind Press.
Damping Factor (Beta) for Wind
Damping Factor (Beta) for Wind
Damping Factor (Beta) for Wind
0.6895
93.3
not Specified
Horizontal
0
0
0.0
Welded
None
RT-1
Y
N
N
N
N
N
N
MPa
°C
mm
mm
°C
NP+EW+WI+FW+BW
NP+EW+EE+FS+BS
NP+OW+WI+FW+BW
NP+OW+EQ+FS+BS
NP+HW+HI
NP+HW+HE
IP+OW+WI+FW+BW
IP+OW+EQ+FS+BS
EP+OW+WI+FW+BW
EP+OW+EQ+FS+BS
HP+HW+HI
HP+HW+HE
IP+WE+EW
IP+WF+CW
IP+VO+OW
IP+VE+EW
NP+VO+OW
FS+BS+IP+OW
FS+BS+EP+OW
Vs Elev.
(Ope)
(Empty)
(Filled)
UBC-94/97
155
C: Open Terrain
1.15
0
0.0
N
0.0100
0.0000
0.0000
Seismic Design Code
UBC Seismic Zone (1=1,2=2a,3=2b,4=3,5=4)
UBC Importance Factor
UBC Seismic Coefficient Ca
UBC Seismic Coefficient Cv
UBC Seismic Coefficient Nv
UBC Horizontal Force Factor
Apply Allowables per paragraph 1612.3.2
UBC 1997
0
1.250
0.360
0.840
1.000
2.000
No
Design Pressure + Static Head
Consider MAP New and Cold in Noz. Design
Consider External Loads for Nozzle Des.
Y
N
Y
km/hr
mm
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Use ASME VIII-1 Appendix 1-9
Material Database Year
Page 5 of 30
Oct 21,2019
N
Current w/Addenda or Code Year
Configuration Directives:
Do not use Nozzle MDMT Interpretation VIII-1 01-37
Use Table G instead of exact equation for "A"
Shell Head Joints are Tapered
Compute "K" in corroded condition
Use Code Case 2286
Use the MAWP to compute the MDMT
For thickness ratios <= 0.35, MDMT will be -155F (-104C)
For PWHT & P1 Materials the MDMT can be < -55F (-48C)
No
Yes
Yes
Yes
No
Yes
Yes
No
Using Metric Material Databases, ASME II D
Calculate B31.3 type stress for Nozzles with Loads
Reduce the MDMT due to lower membrane stress
Consider Longitudinal Stress in MDMT calcs. (Div. 1)
No
Yes
Yes
No
Complete Listing of Vessel Elements and Details:
Element From Node
Element To Node
Element Type
Description
Distance "FROM" to "TO"
Inside Diameter
Element Thickness
Internal Corrosion Allowance
Nominal Thickness
External Corrosion Allowance
Design Internal Pressure
Design Temperature Internal Pressure
Design External Pressure
Design Temperature External Pressure
Effective Diameter Multiplier
Material Name
Allowable Stress, Ambient
Allowable Stress, Operating
Allowable Stress, Hydrotest
Material Density
P Number Thickness
Yield Stress, Operating
UCS-66 Chart Curve Designation
External Pressure Chart Name
UNS Number
Product Form
Efficiency, Longitudinal Seam
Efficiency, Circumferential Seam
Weld is pre-Heated
Element From Node
Detail Type
Detail ID
Dist. from "FROM" Node / Offset dist
Width of Saddle
Height of Saddle at Bottom
Saddle Contact Angle
Height of Composite Ring Stiffener
Width of Wear Plate
Thickness of Wear Plate
Contact Angle, Wear Plate (degrees)
Friction coefficient
Moment Factor
10
20
Cylinder
7500
1670
39
0
0
0
0.6895
93
0.1034
93
1.2
SA-516 70
137.9
137.9
179.27
0.00775
31.75
239.95
B
CS-2
K02700
Plate
1.0
1.0
No
10
Saddle
Saddle
1500
300
1174
120.0
0
350
10
132.0
0.0
3.0
mm
mm
mm
mm
mm
mm
MPa
°C
MPa
°C
MPa
MPa
MPa
kg/cm³
mm
MPa
mm
mm
mm
mm
mm
mm
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Dimension E at base (optional)
Circumferential Eff. over Saddle
Circumferential Eff. at Midspan
Tangent to Tangent dist. (optional)
Element From Node
Detail Type
Detail ID
Dist. from "FROM" Node / Offset dist
Width of Saddle
Height of Saddle at Bottom
Saddle Contact Angle
Height of Composite Ring Stiffener
Width of Wear Plate
Thickness of Wear Plate
Contact Angle, Wear Plate (degrees)
Friction coefficient
Moment Factor
Dimension E at base (optional)
Circumferential Eff. over Saddle
Circumferential Eff. at Midspan
Tangent to Tangent dist. (optional)
4:33pm
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Oct 21,2019
0
1.0
1.0
0
10
Saddle
Sdl 2 Fr10
6000
300
1174
120.0
0
350
10
132.0
0.0
3.0
0
1.0
1.0
0
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mm
mm
mm
mm
mm
mm
mm
mm
mm
mm
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XY Coordinate Calculations:
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XY Coordinate Calculations:
From
10
To
20
X (Horiz.)
mm
7500
Y (Vert.)
mm
...
DX (Horiz.)
mm
DY (Vert.)
mm
7500
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...
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Internal Pressure Calculations:
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Element Thickness, Pressure, Diameter and Allowable Stress :
From
10
To
20
Int. Press
+ Liq. Hd
MPa
Nominal
Thickness
mm
Total Corr
Allowance
mm
Element
Diameter
mm
Allowable
Stress(SE)
MPa
0.6895
...
...
1670
137.9
Design
Pressure
MPa
M.A.W.P.
Corroded
MPa
M.A.P.
New & Cold
MPa
Minimum
Thickness
mm
Required
Thickness
mm
0.6895
6.26526
6.26526
39
4.18756
6.265
6.265
Element Required Thickness and MAWP :
From
10
To
20
Minimum
MAWP: 6.265 MPa, limited by: Cylinder.
Internal Pressure Calculation Results :
ASME Code, Section VIII Division 1, 2017
Cylindrical Shell From 10 To 20 SA-516 70 , UCS-66 Crv. B at 93 °C
Material UNS Number:
K02700
Required Thickness due to Internal Pressure [tr]:
= (P*R)/(S*E-0.6*P) per UG-27 (c)(1)
= (0.69*835)/(137.9*1-0.6*0.69)
= 4.1876 + 0.0000 = 4.1876 mm
Max. Allowable Working Pressure at given Thickness, corroded [MAWP]:
= (S*E*t)/(R+0.6*t) per UG-27 (c)(1)
= (137.9*1*39)/(835+0.6*39)
= 6.265 MPa
Maximum Allowable Pressure, New and Cold [MAPNC]:
= (S*E*t)/(R+0.6*t) per UG-27 (c)(1)
= (137.9*1*39)/(835+0.6*39)
= 6.265 MPa
Actual stress at given pressure and thickness, corroded [Sact]:
= (P*(R+0.6*t))/(E*t)
= (0.69*(835+0.6*39))/(1*39)
= 15.176 MPa
% Elongation per Table UG-79-1 (50*tnom/Rf*(1-Rf/Ro)) 2.282 %
Minimum Design Metal Temperature Results:
Govrn. thk, tg = 39, tr = 39, c = 0 mm, E* = 1
Thickness Ratio = tr * (E*)/(tg - c) = 1, Temp. Reduction = 0 °C
Min Metal Temp. w/o impact per UCS-66, Curve B
Note:
Post Weld Heat Treatment is required for this Element/Joint and it was
specified as being heat treated.
Elements Suitable for Internal Pressure.
11 °C
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Internal Pressure Calculations:
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External Pressure Calculations:
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External Pressure Calculation Results :
External Pressure Calculations:
From
10
To
20
Section
Length
mm
Outside
Diameter
mm
Corroded
Thickness
mm
7500
1748
39
Factor
A
Factor
B
MPa
0.00092436
82.8451
External Pressure Calculations:
From
10
To
20
External
Actual T.
mm
External
Required T.
mm
39
External
Design Pressure
MPa
External
M.A.W.P.
MPa
0.10343
2.4645
10.2843
Minimum
2.464
External Pressure Calculations:
From
10
To
20
Actual Length
Bet. Stiffeners
mm
Allowable Length
Bet. Stiffeners
mm
Ring Inertia
Required
mm**4
Ring Inertia
Available
mm**4
7500
589085
No Calc
No Calc
Elements Suitable for External Pressure.
ASME Code, Section VIII Division 1, 2017
Cylindrical Shell From 10 to 20 Ext. Chart: CS-2 at 93 °C
Elastic Modulus from Chart: CS-2 at 93 °C
: 0.200E+06 MPa
Results for Maximum Allowable External Pressure (MAEP):
Tca
OD
SLEN
D/t
L/D
Factor A
39.000
1748.00
7500.00
44.82
4.2906 0.0009244
EMAP = (4*B)/(3*(D/t)) = (4*82.85 )/(3*44.82 ) = 2.464 MPa
B
82.85
Results for Required Thickness (Tca):
Tca
OD
SLEN
D/t
L/D
Factor A
10.284
1748.00
7500.00
169.97
4.2906 0.0001319
EMAP = (4*B)/(3*(D/t)) = (4*13.18 )/(3*170 ) = 0.103 MPa
B
13.18
Results for Maximum Stiffened Length (Slen):
Tca
OD
SLEN
D/t
L/D
Factor A
39.000
1748.00
589085.12
44.82
50.0000 0.0005581
EMAP = (4*B)/(3*(D/t)) = (4*55.8 )/(3*44.82 ) = 1.66 MPa
B
55.80
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Element and Detail Weights:
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Element and Detail Weights:
Element
Volume
ltr
Corroded
Metal Wgt.
kgm
Corroded
ID Volume
ltr
Extra due
Misc %
kgm
12171.6
16430.9
12171.6
16430.9
...
12171
16430.92
12171
16430.92
0
From Type
Weight of
Detail
kgm
X Offset,
Dtl. Cent.
mm
Y Offset,
Dtl. Cent.
mm
10 Sadl
10 Sadl
289.775
289.775
1500
6000
980
980
From
To
10
Element
Metal Wgt.
kgm
20
Total
ID
Weight of Details:
Description
Saddle
Sdl 2 Fr10
Total Weight of Each Detail Type:
Saddles
579.5
Sum of the Detail Weights
579.5 kgm
Weight Summation Results: (kgm)
Fabricated
Shop Test
Shipping
Erected
Empty
Operating
Main Elements
Saddles
Test Liquid
12171.6
579.5
...
12171.6
579.5
16420.9
12171.6
579.5
...
12171.6
579.5
...
12171.6
579.5
...
12171.6
579.5
...
Totals
12751.2
29172.0
12751.2
12751.2
12751.2
12751.2
Weight Summary:
Fabricated Wt.
Shop Test Wt.
Shipping Wt.
Erected Wt.
Ope. Wt. no Liq
Operating Wt.
Oper. Wt. + CA
Field Test Wt.
-
Bare Weight without Removable Internals
Fabricated Weight + Water ( Full )
Fab. Weight + removable Intls.+ Shipping App.
Fab. Wt + or - loose items (trays,platforms etc.)
Fab. Weight + Internals. + Details + Weights
Empty Weight + Operating Liq. Uncorroded
Corr Wt. + Operating Liquid
Empty Weight + Water (Full)
Note:
The Corroded Weight and thickness are used in the Horizontal
Vessel Analysis (Ope Case) and Earthquake Load Calculations.
Outside Surface Areas of Elements:
From
To
10
Total
20
Surface
Area
mm²
41186280
41186280.000 mm²
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12751.2
29172.0
12751.2
12751.2
12751.2
12751.2
12751.2
29172.0
kgm
kgm
kgm
kgm
kgm
kgm
kgm
kgm
® SPLM Licensed User
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Wind Load Calculation:
Step:
6
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4:33pm
Page 12 of 30
Oct 21,2019
Wind Analysis Results per UBC 1994 or UBC 1997
Importance Factor as Entered by the User is
Wind Stagnation Pressure (qs) from Table 16-F
Pressure Coefficient from Table 16-H
User Entered Basic Wind Speed
1.150
1.1
Cq 0.800
155.0
kPa
km/hr
P(height) = Ce(height,Exp) * Cq * qs * Imp Fact. [18-1](1994) or [20-1](1997)
The values of Ce are shown as the in the table below:
Element
Ce
From: 10
1.0600
Wind Load Calculation:
From
10
To
20
Wind
Height
mm
Wind
Diameter
mm
Wind
Area
mm²
Wind
Pressure
kPa
Element
Wind Load
N
1174
2097.6
15732003
1.11006
17463.1
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Earthquake Load Calculation:
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Earthquake Analysis Results per UBC 1997
The
The
The
The
The
The
The
UBC Zone Factor for the Vessel is .............
Importance Factor as Specified by the User is
UBC Force Factor as Specified by the User is ..
UBC Total Weight (W) for the Vessel is ........
UBC Total Shear (V) for the Vessel is .........
UBC Seismic Coefficient Value Ca is ...........
UBC Seismic Coefficient Value Cv is ...........
0.0000
1.250
2.000
125037.8
28122.2
0.360
0.840
N
N
Note: The base shear printed above has been modified
by the user defined Earthquake scalar.
Calculation Steps for Computing the design Base Shear (V) per UBC 1997
Computation of V per equation (34-1):
V = 0.7 * Ca * I * W
V = 0.7 * 0.36 * 1.25 * 125038
V = 39386.9 N
Computation of V per equation (30-5):
V = 2.5 * Ca * I * W / R
V = 2.5 * 0.36 * 1.25 * 125038/2
V = 70333.8 N
The computed base shear is the minimum of V from 34-1 and 30-5.
Computation of V per equation (34-2), minimum V. V cannot be less than
this value !
V = 0.56 * Ca * I * W
V = 0.56 * 0.36 * 1.25 * 125038
V = 31509.5 N
Total Adjusted Base Shear V:
= V * Scalar Multiplier = 39386.9 * 0.7140 = 28122.2 N
Next Sum the earthquake weights times their heights (wi*hi):
Current Sum = Prev. Sum + Wght 41679. * Hght 835.000 = 34816292.
Current Sum = Prev. Sum + Wght 41679. * Hght 835.000 = 69632584.
Current Sum = Prev. Sum + Wght 41679. * Hght 835.000 = 104448880.
Compute the load at each level based on equation 30-15 and multiply
by the load case scalar. The sum will be the total adjusted shear.
Fx
Fx
Fx
Fx
=
=
=
=
( V * wx * hx / ( sum of ( wi * hi ))) * EqFact
[(39387.) * 41679. * 835.000 / 104448880.]*.7140 = 9374.
[(39387.) * 41679. * 835.000 / 104448880.]*.7140 = 9374.
[(39387.) * 41679. * 835.000 / 104448880.]*.7140 = 9374.
Earthquake Load Calculation:
From
To
10 Sadl
Sadl
20
10
20
Earthquake
Height
mm
Earthquake
Weight
N
Element
Ope Load
N
835
835
835
41679.3
41679.3
41679.3
9374.08
9374.08
9374.08
Note:
The Earthquake Loads calculated and printed in the Earthquake
Load calculation report have been factored by the input
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Earthquake Load Calculation:
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scalar/load reduction factor of: 0.714.
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Center of Gravity Calculation:
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8
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Oct 21,2019
Shop/Field Installation Options :
Note : The CG is computed from the first Element From Node
Center of Gravity of Saddles
3750.000 mm
Center of Gravity of Bare Shell New and Cold
Center of Gravity of Bare Shell Corroded
3750.000 mm
3750.000 mm
Vessel CG in the Operating Condition
Vessel CG in the Fabricated (Shop/Empty) Condition
Vessel CG in the Test Condition
3750.000 mm
3750.000 mm
3750.000 mm
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Horizontal Vessel Analysis (Ope.):
Step:
9
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Oct 21,2019
ASME Horizontal Vessel Analysis: Stresses for the Left Saddle
(per ASME Sec. VIII Div. 2 based on the Zick method.)
Horizontal Vessel Stress Calculations : Operating Case
Note:
Wear Pad Width (350.00) is less than 1.56*sqrt(rm*t)
and less than 2a. The wear plate will be ignored.
Minimum Wear Plate Width to be considered in analysis [b1]:
= min( b + 1.56*sqrt( Rm * t ), 2a )
= min( 300 + 1.56*sqrt( 854.5 * 39 ), 2 * 470 )
= 584.7822 mm
Input and Calculated Values:
Vessel Mean Radius
Stiffened Vessel Length per 4.15.6
Distance from Saddle to Vessel tangent
Saddle Width
Saddle Bearing Angle
Rm
L
a
854.50
7500.00
470.00
b
theta
300.00
120.00
mm
degrees
137.90
0.00
1.00
1.00
MPa
MPa
Shell Allowable Stress used in Calculation
Head Allowable Stress used in Calculation
Circumferential Efficiency in Plane of Saddle
Circumferential Efficiency at Mid-Span
Saddle Force Q, Operating Case
Horizontal Vessel Analysis Results:
92021.56
mm
mm
mm
N
Actual
MPa
Allowable
MPa
Midspan
Midspan
Saddles
Saddles
6.06
9.05
7.37
7.66
137.90
137.90
137.90
137.90
Tangential Shear in Shell
Circ. Stress at Horn of Saddle
Circ. Compressive Stress in Shell
2.83
2.57
0.31
110.32
172.38
137.90
Long.
Long.
Long.
Long.
Stress
Stress
Stress
Stress
at
at
at
at
Top
Bottom
Top
Bottom
of
of
of
of
Intermediate Results: Saddle Reaction Q due to Wind or Seismic
Saddle Reaction Force due to Wind Ft [Fwt]:
= Ftr * ( Ft/Num of Saddles + Z Force Load ) * B / E
= 3 * ( 17463/2 + 0 ) * 1174/1531
= 20084.8 N
Saddle Reaction Force due to Wind Fl or Friction [Fwl]:
= max( Fl, Friction Load, Sum of X Forces) * B / Ls
= max( 3197, 0, 0 ) * 1174/4500
= 834.0 N
Saddle Reaction Force due to Earthquake Fl or Friction [Fsl]:
= max( Fl, Friction Force, Sum of X Forces ) * B / Ls
= max( 28122, 0, 0 ) * 1174/4500
= 7336.8 N
Saddle Reaction Force due to Earthquake Ft [Fst]:
= Ftr * ( Ft/Num of Saddles + Z Force Load ) * B / E
= 3 * ( 28122/2 + 0 ) * 1174/1531
= 32344.2 N
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Horizontal Vessel Analysis (Ope.):
Step:
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Oct 21,2019
Load Combination Results for Q + Wind or Seismic [Q]:
= Saddle Load + Max( Fwl, Fwt, Fsl, Fst )
= 59677 + Max( 834, 20085, 7337, 32344 )
= 92021.6 N
Summary of Loads at the base of this Saddle:
Vertical Load (including saddle weight)
Transverse Shear Load Saddle
Ft
Longitudinal Shear Load Saddle
94863.09
14061.12
28122.25
N
N
N
Formulas and Substitutions for Horizontal Vessel Analysis:
Note: Wear Plate is Welded to the Shell, k = 0.1
The Computed K values from Table 4.15.1:
K1 = 0.1066
K2 = 1.1707
K5 = 0.7603
K6 = 0.0529
K9 = 0.2711
K10 = 0.0581
K3 = 0.8799
K7 = 0.0172
K1* = 0.1923
K4
K8
= 0.4011
= 0.3405
Note: Dimension a is greater than or equal to Rm / 2.
Moment per Equation 4.15.3 [M1]:
= -Q*a [1 - (1- a/L + (R²-h2²)/(2a*L))/(1+(4h2)/3L)]
= -92022*470[1-(1-470/7500+(854.5²-0²)/
(2*470*7500))/(1+(4*0)/(3*7500))]
= 1769802.0 N-mm
Moment per Equation 4.15.4 [M2]:
= Q*L/4(1+2(R²-h2²)/(L²))/(1+(4h2)/( 3L))-4a/L
= 92022*7500/4(1+2(854.5²-0²)/(7500²))/(1+(4*0)/
(3*7500))-4*470/7500
= 133823976.0 N-mm
Longitudinal Stress at Top of Shell (4.15.6) [Sigma1]:
= P * Rm/(2t) - M2/(pi*Rm²t)
= 0.69 * 854.5/(2*39 ) - 133823976/(pi*854.5²*39 )
= 6.06 MPa
Longitudinal Stress at Bottom of Shell (4.15.7) [Sigma2]:
= P * Rm/(2t) + M2/(pi * Rm² * t)
= 0.69 * 854.5/(2 * 39 ) + 133823976/(pi * 854.5² * 39 )
= 9.05 MPa
Longitudinal Stress at Top of Shell at Support (4.15.10) [Sigma*3]:
= P * Rm/(2t) - M1/(K1*pi*Rm²t)
= 0.69*854.5/(2*39)-1769802/(0.107*pi*854.5²*39)
= 7.37 MPa
Longitudinal Stress at Bottom of Shell at Support (4.15.11) [Sigma*4]:
= P * Rm/(2t) + M1/(K1* * pi * Rm² * t)
= 0.69*854.5/(2*39)+1769802/(0.192*pi*854.5²*39)
= 7.66 MPa
Maximum Shear Force in the Saddle (4.15.5) [T]:
= Q(L-2a)/(L+(4*h2/3))
= 92022 ( 7500 - 2 * 470 )/(7500 + ( 4 * 0/3))
= 80488.2 N
Shear Stress in the shell no rings, not stiffened (4.15.14) [tau2]:
= K2 * T / ( Rm * t )
= 1.171 * 80488/( 854.5 * 39 )
= 2.83 MPa
Decay Length (4.15.22) [x1,x2]:
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= 0.78 * sqrt( Rm * t )
= 0.78 * sqrt( 854.5 * 39 )
= 142.391 mm
Circumferential Stress in shell, no rings (4.15.23) [sigma6]:
= -K5 * Q * k / ( t * ( b + X1 + X2 ) )
= -0.76 * 92022 * 0.1/( 39 * ( 300 + 142.4 + 142.4 ) )
= -0.31 MPa
Circ. Comp. Stress at Horn of Saddle, L>=8Rm (4.15.24) [sigma7]:
= -Q/(4*t*(b+X1+X2)) - 3*K7*Q/(2*t²)
= -92022/(4*39 *(300 +142.4 +142.4 )) 3*0.0172 *92022/(2*39²)
= -2.57 MPa
Effective reinforcing plate width (4.15.1) [B1]:
= min( b + 1.56 * sqrt( Rm * t ), 2a )
= min( 300 + 1.56 * sqrt( 854.5 * 39 ), 2 * 470 )
= 584.78 mm
Free Un-Restrained Thermal Expansion between the Saddles [Exp]:
= Alpha * Ls * ( Design Temperature - Ambient Temperature )
= 0.12059E-04 * 4500 * ( 93.34 - 21.11 )
= 3.919 mm
Results for Vessel Ribs, Web and Base:
Baseplate Length
Baseplate Thickness
Baseplate Width
Number of Ribs ( inc. outside ribs )
Rib Thickness
Web Thickness
Web Location
Saddle Yield Stress
Height of Web at Center
Friction Coefficient
Bplen
Bpthk
Bpwid
Nribs
Ribtk
Webtk
Webloc
Sy
Hw,c
mu
1900.0001
26.0000
300.0000
4
10.0000
10.0000
Center
248.2
306.0
0.000
mm
mm
mm
mm
mm
MPa
mm
Note: In the tables below Io is I for the rectangle + Area * Centroid Distance^2
Moment of Inertia of Saddle - Transverse Direction (90 degrees to long axis)
Shell
Wearplate
Web
BasePlate
Totals
B
D
Y
A
AY
Io
631.5
350.0
10.0
300.0
...
39.0
10.0
264.0
26.0
...
19.5
44.0
181.0
326.0
...
24629.0
3500.0
2640.0
7800.0
38569.0
480266.4
154000.0
477840.0
2542800.0
3654906.5
0.143E+09
0.905E+07
0.350E+08
0.418E+09
0.604E+09
Distance to Centroid [C1]:
= AY / A
= 143894/38569
= 94.763 mm
Angle [beta]:
= 180 - Saddle Angle/2
= 180 - 120/2
= 120.0
Saddle Splitting Coefficient [K1]:
= ( 1 + cos(beta) - 0.5*sin(beta)² )/(pi - beta + sin(beta)cos(beta) )
= ( 1 + cos(120 ) - 0.5*sin(120 )² )/(pi - 2.094 + sin(120 )cos(120 ) )
= 0.2035
Saddle Splitting Force [Fh]:
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= K1 * Q
= 0.204 * 92022
= 18728.3828 N
Tension Stress, St = ( Fh/As )
=
Allowed Stress, Sa = 0.6 * Yield Str =
1.3436
148.9320
MPa
MPa
Saddle Splitting Dimension [d]:
= B - R * sin( theta )/ theta
= 1174 - 835 * sin( 1.047 )/1.047
= 483.461 mm
Bending Moment, M
= Fh * d
=
9058106.0000
Bending Stress, Sb = ( M * C1 / I ) =
Allowed Stress, Sa = 2/3 * Yield Str =
1.4203
165.4800
N-mm
MPa
MPa
Minimum Thickness of Baseplate per Moss:
= ( 3( Q + Saddle_Wt )BasePlateWidth / ( 4 * BasePlateLength * AllStress ))½
= ( 3(92022 + 2842 )300/( 4 * 1900 * 165.5 ))½
= 8.240 mm
Calculation of Axial Load, Intermediate Values and Compressive Stress:
Web Length Dimension [ Web Length ]:
= 2 * cos( 90 - Saddle Angle/2 )( Inside Radius + Shell Thk + Wear Plate Thk )
= 2 * cos( 90 - 120/2 )( 835 + 39 + 10 )
= 1531.133 mm
Distance between Ribs [e]:
= Web Length / ( Nribs - 1 )
= 1531/( 4 - 1 )
= 510.378 mm
Baseplate Pressure Area [Ap]:
= e * Bpwid / 2
= 510.4 * 300/2
= 76556.641 mm²
Axial Load [P]:
= Ap * Bp
= 76557 * 0.161
= 12359.405 N
Area of the Rib and Web [Ar]:
= Rib Area + Web Area
= 2900 + 2552
= 5451.888 mm²
Compressive Stress [Sc]:
= P/Ar
= 12359/5452
= 2.267 MPa
Check of Outside Ribs:
Inertia of Saddle, Outer Ribs - Longitudinal Direction
Rib+Web
B
D
Y
A
AY
Io
10.0
300.0
...
3000.0
...
0.225E+08
Rib dimension [D]:
= Saddle Width - Web Thickness
= 300 - 10
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= 290.000 mm
Distance to Centroid from Datum [ytot]:
= AY / A
= 0/5452
= 0.000 mm
Distance to Centroid [C1]:
= Saddle Width / 2
= 300/2
= 150.000 mm
Radius of Gyration [r]:
= sqrt( Total Inertia / Total Area )
= sqrt( 22499978/5452 )
= 64.242 mm
Length of Outer Rib [L]:
= Saddle Height - cos( theta/2 )( radius + shlthk + wpdthk ) - bpthk
= 1174 - cos( 120/2 )( 835 + 39 + 10 ) - 26
= 706.000 mm
Intermediate Term [Cc]:
= sqrt( 2 * pi² * Elastic Modulus / Yield Stress )
= sqrt( 2 * pi² * 199955/248.2 )
= 126.099
Slenderness ratio [KL/r]:
= KL/r
= 1 * 706/64.24
= 10.990
Bending Moment [Rm]:
= Fl /( 2 * Bplen ) * e * L / 2
= 28122/( 2 * 1900 ) * 510.4 * 706/2
= 1333855.625 N-mm
Compressive Allowable, KL/r < Cc ( 10.99 < 126.1 ) per AISC E2-1 [Sca]:
= ( 1-(Klr)²/(2*Cc²))Fy/(5/3+3*(Klr)/(8*Cc)-(Klr³)/(8*Cc³)
= ( 1-( 10.99 )²/(2 * 126.1² ))248.2/
( 5/3+3*(10.99 )/(8* 126.1 )-( 10.99³)/(8*126.1³)
= 145.5 MPa
AISC Unity Check of Outside Ribs ( must be <= 1 )
= Sc/Sca + ( Rm * C1 / I )/Sba
= 2.267/145.5 + ( 1333855 * 150/22500000 )/165.5
= 0.069
Check of Inside Ribs:
Inertia of Saddle, Inner Ribs - Axial Direction
Rib
Web
Totals
B
D
Y
A
AY
Io
10.0
510.4
...
290.0
10.0
...
0.0
0.0
...
2900.0
5103.8
8003.8
0.0
0.0
...
0.225E+08
0.425E+05
0.225E+08
Distance to Centroid from Datum [ytot]:
= AY / A
= 0/8004
= 0.000 mm
Distance to Centroid [C1]:
= Saddle Width / 2
= 300/2
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= 150.000 mm
Length of Inner Rib [L]:
= Saddle Height - sqrt( (Ro + Wpdthk)^2 - (Pitch/2)^2 ) - Bpthk
= 1174 - sqrt( (884 + 10 )^2 - (510.4/2)^2 ) - 26
= 301.634 mm
Radius of Gyration [r]:
= sqrt( Total Inertia / Total Area )
= sqrt( 22541676/8004 )
= 53.070 mm
Slenderness ratio [KL/r]:
= KL/r
= 1 * 301.6/53.07
= 5.684
Unit Force [Force,u]:
= Fl / ( 2 * Baseplate Length )
= 28122/( 2 * 1900 )
= 7.401 N/mm
Moment at base of inner Rib [Mbase,c]:
= Unit Force * e * L
= 7.401 * 510.4 * 301.6
= 1139764.250 N-mm
Bending Stress due to Transverse Force and Weight Load [SigmaB,base,c]:
= Bending Moment / Section Modulus
= 1139764/150278
= 7.582 MPa
Compressive Allowable, KL/r < Cc ( 5.684 < 126.1 ) per AISC E2-1 [Sca]:
= ( 1-(Klr)²/(2*Cc²))Fy/(5/3+3*(Klr)/(8*Cc)-(Klr³)/(8*Cc³)
= ( 1-( 5.684 )²/(2 * 126.1² ))248.2/
( 5/3+3*(5.684 )/(8* 126.1 )-( 5.684³)/(8*126.1³)
= 147.3 MPa
AISC Unity Check of Inside Ribs ( must be <= 1 )
= Sc/Sca + ( Mbase,c * C1/I )/Sba
= 3.19/147.3 + ( 1139764 * 150/22541676 )/165.5
= 0.067
ASME Horizontal Vessel Analysis: Stresses for the Right Saddle
(per ASME Sec. VIII Div. 2 based on the Zick method.)
Note:
Wear Pad Width (350.00) is less than 1.56*sqrt(rm*t)
and less than 2a. The wear plate will be ignored.
Minimum Wear Plate Width to be considered in analysis [b1]:
= min( b + 1.56*sqrt( Rm * t ), 2a )
= min( 300 + 1.56*sqrt( 854.5 * 39 ), 2 * 470 )
= 584.7822 mm
Input and Calculated Values:
Vessel Mean Radius
Stiffened Vessel Length per 4.15.6
Distance from Saddle to Vessel tangent
Saddle Width
Saddle Bearing Angle
Shell Allowable Stress used in Calculation
Rm
L
a
854.50
7500.00
470.00
mm
mm
mm
b
theta
300.00
120.00
mm
degrees
137.90
MPa
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Head Allowable Stress used in Calculation
Circumferential Efficiency in Plane of Saddle
Circumferential Efficiency at Mid-Span
Saddle Force Q, Operating Case
Page 22 of 30
Oct 21,2019
0.00
1.00
1.00
92021.57
Horizontal Vessel Analysis Results:
MPa
N
Actual
MPa
Allowable
MPa
Midspan
Midspan
Saddles
Saddles
6.06
9.05
7.37
7.66
137.90
137.90
137.90
137.90
Tangential Shear in Shell
Circ. Stress at Horn of Saddle
Circ. Compressive Stress in Shell
2.83
2.57
0.31
110.32
172.38
137.90
Long.
Long.
Long.
Long.
Stress
Stress
Stress
Stress
at
at
at
at
Top
Bottom
Top
Bottom
of
of
of
of
Intermediate Results: Saddle Reaction Q due to Wind or Seismic
Saddle Reaction Force due to Wind Ft [Fwt]:
= Ftr * ( Ft/Num of Saddles + Z Force Load ) * B / E
= 3 * ( 17463/2 + 0 ) * 1174/1531
= 20084.8 N
Saddle Reaction Force due to Wind Fl or Friction [Fwl]:
= max( Fl, Friction Load, Sum of X Forces) * B / Ls
= max( 3197, 0, 0 ) * 1174/4500
= 834.0 N
Saddle Reaction Force due to Earthquake Fl or Friction [Fsl]:
= max( Fl, Friction Force, Sum of X Forces ) * B / Ls
= max( 28122, 0, 0 ) * 1174/4500
= 7336.8 N
Saddle Reaction Force due to Earthquake Ft [Fst]:
= Ftr * ( Ft/Num of Saddles + Z Force Load ) * B / E
= 3 * ( 28122/2 + 0 ) * 1174/1531
= 32344.2 N
Load Combination Results for Q + Wind or Seismic [Q]:
= Saddle Load + Max( Fwl, Fwt, Fsl, Fst )
= 59677 + Max( 834, 20085, 7337, 32344 )
= 92021.6 N
Summary of Loads at the base of this Saddle:
Vertical Load (including saddle weight)
Transverse Shear Load Saddle
Ft
Longitudinal Shear Load Saddle
94863.10
14061.12
28122.25
N
N
N
Formulas and Substitutions for Horizontal Vessel Analysis:
Note: Wear Plate is Welded to the Shell, k = 0.1
The Computed K values from Table 4.15.1:
K1 = 0.1066
K2 = 1.1707
K5 = 0.7603
K6 = 0.0529
K9 = 0.2711
K10 = 0.0581
K3 = 0.8799
K7 = 0.0172
K1* = 0.1923
K4
K8
Note: Dimension a is greater than or equal to Rm / 2.
Moment per Equation 4.15.3 [M1]:
= -Q*a [1 - (1- a/L + (R²-h2²)/(2a*L))/(1+(4h2)/3L)]
= -92022*470[1-(1-470/7500+(854.5²-0²)/
= 0.4011
= 0.3405
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(2*470*7500))/(1+(4*0)/(3*7500))]
= 1769802.2 N-mm
Moment per Equation 4.15.4 [M2]:
= Q*L/4(1+2(R²-h2²)/(L²))/(1+(4h2)/( 3L))-4a/L
= 92022*7500/4(1+2(854.5²-0²)/(7500²))/(1+(4*0)/
(3*7500))-4*470/7500
= 133823984.0 N-mm
Longitudinal Stress at Top of Shell (4.15.6) [Sigma1]:
= P * Rm/(2t) - M2/(pi*Rm²t)
= 0.69 * 854.5/(2*39 ) - 133823984/(pi*854.5²*39 )
= 6.06 MPa
Longitudinal Stress at Bottom of Shell (4.15.7) [Sigma2]:
= P * Rm/(2t) + M2/(pi * Rm² * t)
= 0.69 * 854.5/(2 * 39 ) + 133823984/(pi * 854.5² * 39 )
= 9.05 MPa
Longitudinal Stress at Top of Shell at Support (4.15.10) [Sigma*3]:
= P * Rm/(2t) - M1/(K1*pi*Rm²t)
= 0.69*854.5/(2*39)-1769802/(0.107*pi*854.5²*39)
= 7.37 MPa
Longitudinal Stress at Bottom of Shell at Support (4.15.11) [Sigma*4]:
= P * Rm/(2t) + M1/(K1* * pi * Rm² * t)
= 0.69*854.5/(2*39)+1769802/(0.192*pi*854.5²*39)
= 7.66 MPa
Maximum Shear Force in the Saddle (4.15.5) [T]:
= Q(L-2a)/(L+(4*h2/3))
= 92022 ( 7500 - 2 * 470 )/(7500 + ( 4 * 0/3))
= 80488.2 N
Shear Stress in the shell no rings, not stiffened (4.15.14) [tau2]:
= K2 * T / ( Rm * t )
= 1.171 * 80488/( 854.5 * 39 )
= 2.83 MPa
Decay Length (4.15.22) [x1,x2]:
= 0.78 * sqrt( Rm * t )
= 0.78 * sqrt( 854.5 * 39 )
= 142.391 mm
Circumferential Stress in shell, no rings (4.15.23) [sigma6]:
= -K5 * Q * k / ( t * ( b + X1 + X2 ) )
= -0.76 * 92022 * 0.1/( 39 * ( 300 + 142.4 + 142.4 ) )
= -0.31 MPa
Circ. Comp. Stress at Horn of Saddle, L>=8Rm (4.15.24) [sigma7]:
= -Q/(4*t*(b+X1+X2)) - 3*K7*Q/(2*t²)
= -92022/(4*39 *(300 +142.4 +142.4 )) 3*0.0172 *92022/(2*39²)
= -2.57 MPa
Effective reinforcing plate width (4.15.1) [B1]:
= min( b + 1.56 * sqrt( Rm * t ), 2a )
= min( 300 + 1.56 * sqrt( 854.5 * 39 ), 2 * 470 )
= 584.78 mm
Results for Vessel Ribs, Web and Base:
Baseplate Length
Baseplate Thickness
Baseplate Width
Bplen
Bpthk
Bpwid
1900.0001
26.0000
300.0000
mm
mm
mm
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Number of Ribs ( inc. outside ribs )
Rib Thickness
Web Thickness
Web Location
Saddle Yield Stress
Height of Web at Center
Friction Coefficient
4:33pm
Nribs
Ribtk
Webtk
Webloc
Sy
Hw,c
mu
Page 24 of 30
Oct 21,2019
4
10.0000
10.0000
Center
248.2
306.0
0.000
mm
mm
MPa
mm
Note: In the tables below Io is I for the rectangle + Area * Centroid Distance^2
Moment of Inertia of Saddle - Transverse Direction (90 degrees to long axis)
Shell
Wearplate
Web
BasePlate
Totals
B
D
Y
A
AY
Io
631.5
350.0
10.0
300.0
...
39.0
10.0
264.0
26.0
...
19.5
44.0
181.0
326.0
...
24629.0
3500.0
2640.0
7800.0
38569.0
480266.4
154000.0
477840.0
2542800.0
3654906.5
0.143E+09
0.905E+07
0.350E+08
0.418E+09
0.604E+09
Distance to Centroid [C1]:
= AY / A
= 143894/38569
= 94.763 mm
Angle [beta]:
= 180 - Saddle Angle/2
= 180 - 120/2
= 120.0
Saddle Splitting Coefficient [K1]:
= ( 1 + cos(beta) - 0.5*sin(beta)² )/(pi - beta + sin(beta)cos(beta) )
= ( 1 + cos(120 ) - 0.5*sin(120 )² )/(pi - 2.094 + sin(120 )cos(120 ) )
= 0.2035
Saddle Splitting Force [Fh]:
= K1 * Q
= 0.204 * 92022
= 18728.3848 N
Tension Stress, St = ( Fh/As )
=
Allowed Stress, Sa = 0.6 * Yield Str =
1.3436
148.9320
MPa
MPa
Saddle Splitting Dimension [d]:
= B - R * sin( theta )/ theta
= 1174 - 835 * sin( 1.047 )/1.047
= 483.461 mm
Bending Moment, M
= Fh * d
=
9058107.0000
Bending Stress, Sb = ( M * C1 / I ) =
Allowed Stress, Sa = 2/3 * Yield Str =
1.4203
165.4800
N-mm
MPa
MPa
Minimum Thickness of Baseplate per Moss:
= ( 3( Q + Saddle_Wt )BasePlateWidth / ( 4 * BasePlateLength * AllStress ))½
= ( 3(92022 + 2842 )300/( 4 * 1900 * 165.5 ))½
= 8.240 mm
Calculation of Axial Load, Intermediate Values and Compressive Stress:
Web Length Dimension [ Web Length ]:
= 2 * cos( 90 - Saddle Angle/2 )( Inside Radius + Shell Thk + Wear Plate Thk )
= 2 * cos( 90 - 120/2 )( 835 + 39 + 10 )
= 1531.133 mm
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Distance between Ribs [e]:
= Web Length / ( Nribs - 1 )
= 1531/( 4 - 1 )
= 510.378 mm
Baseplate Pressure Area [Ap]:
= e * Bpwid / 2
= 510.4 * 300/2
= 76556.641 mm²
Axial Load [P]:
= Ap * Bp
= 76557 * 0.161
= 12359.407 N
Area of the Rib and Web [Ar]:
= Rib Area + Web Area
= 2900 + 2552
= 5451.888 mm²
Compressive Stress [Sc]:
= P/Ar
= 12359/5452
= 2.267 MPa
Check of Outside Ribs:
Inertia of Saddle, Outer Ribs - Longitudinal Direction
Rib+Web
B
D
Y
A
AY
Io
10.0
300.0
...
3000.0
...
0.225E+08
Rib dimension [D]:
= Saddle Width - Web Thickness
= 300 - 10
= 290.000 mm
Distance to Centroid from Datum [ytot]:
= AY / A
= 0/5452
= 0.000 mm
Distance to Centroid [C1]:
= Saddle Width / 2
= 300/2
= 150.000 mm
Radius of Gyration [r]:
= sqrt( Total Inertia / Total Area )
= sqrt( 22499978/5452 )
= 64.242 mm
Length of Outer Rib [L]:
= Saddle Height - cos( theta/2 )( radius + shlthk + wpdthk ) - bpthk
= 1174 - cos( 120/2 )( 835 + 39 + 10 ) - 26
= 706.000 mm
Intermediate Term [Cc]:
= sqrt( 2 * pi² * Elastic Modulus / Yield Stress )
= sqrt( 2 * pi² * 199955/248.2 )
= 126.099
Slenderness ratio [KL/r]:
= KL/r
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= 1 * 706/64.24
= 10.990
Bending Moment [Rm]:
= Fl /( 2 * Bplen ) * e * L / 2
= 28122/( 2 * 1900 ) * 510.4 * 706/2
= 1333855.625 N-mm
Compressive Allowable, KL/r < Cc ( 10.99 < 126.1 ) per AISC E2-1 [Sca]:
= ( 1-(Klr)²/(2*Cc²))Fy/(5/3+3*(Klr)/(8*Cc)-(Klr³)/(8*Cc³)
= ( 1-( 10.99 )²/(2 * 126.1² ))248.2/
( 5/3+3*(10.99 )/(8* 126.1 )-( 10.99³)/(8*126.1³)
= 145.5 MPa
AISC Unity Check of Outside Ribs ( must be <= 1 )
= Sc/Sca + ( Rm * C1 / I )/Sba
= 2.267/145.5 + ( 1333855 * 150/22500000 )/165.5
= 0.069
Check of Inside Ribs:
Inertia of Saddle, Inner Ribs - Axial Direction
Rib
Web
Totals
B
D
Y
A
AY
Io
10.0
510.4
...
290.0
10.0
...
0.0
0.0
...
2900.0
5103.8
8003.8
0.0
0.0
...
0.225E+08
0.425E+05
0.225E+08
Distance to Centroid from Datum [ytot]:
= AY / A
= 0/8004
= 0.000 mm
Distance to Centroid [C1]:
= Saddle Width / 2
= 300/2
= 150.000 mm
Length of Inner Rib [L]:
= Saddle Height - sqrt( (Ro + Wpdthk)^2 - (Pitch/2)^2 ) - Bpthk
= 1174 - sqrt( (884 + 10 )^2 - (510.4/2)^2 ) - 26
= 301.634 mm
Radius of Gyration [r]:
= sqrt( Total Inertia / Total Area )
= sqrt( 22541676/8004 )
= 53.070 mm
Slenderness ratio [KL/r]:
= KL/r
= 1 * 301.6/53.07
= 5.684
Unit Force [Force,u]:
= Fl / ( 2 * Baseplate Length )
= 28122/( 2 * 1900 )
= 7.401 N/mm
Moment at base of inner Rib [Mbase,c]:
= Unit Force * e * L
= 7.401 * 510.4 * 301.6
= 1139764.250 N-mm
Bending Stress due to Transverse Force and Weight Load [SigmaB,base,c]:
= Bending Moment / Section Modulus
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Horizontal Vessel Analysis (Ope.):
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= 1139764/150278
= 7.582 MPa
Compressive Allowable, KL/r < Cc ( 5.684 < 126.1 ) per AISC E2-1 [Sca]:
= ( 1-(Klr)²/(2*Cc²))Fy/(5/3+3*(Klr)/(8*Cc)-(Klr³)/(8*Cc³)
= ( 1-( 5.684 )²/(2 * 126.1² ))248.2/
( 5/3+3*(5.684 )/(8* 126.1 )-( 5.684³)/(8*126.1³)
= 147.3 MPa
AISC Unity Check of Inside Ribs ( must be <= 1 )
= Sc/Sca + ( Mbase,c * C1/I )/Sba
= 3.19/147.3 + ( 1139764 * 150/22541676 )/165.5
= 0.067
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MDMT Summary:
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Minimum Design Metal Temperature Results Summary :
Curve
Description
Notes
[8]
B
Warmest MDMT:
Basic
MDMT
°C
Reduced
MDMT
°C
11
11
11
11
UG-20(f)
MDMT
°C
Thickness
ratio
Gov
Thk
mm
E*
PWHT
reqd
1.000
39.000
1.00
Yes
Required Minimum Design Metal Temperature
Warmest Computed Minimum Design Metal Temperature
0.0
11.0
Warning: Computed overall MDMT was higher than the required value !
Notes:
[ ! ] - This was an impact tested material.
[ 1] - Governing Nozzle Weld.
[ 4] - ANSI Flange MDMT Calcs; Thickness ratio per UCS-66(b)(1)(-c).
[ 5] - ANSI Flange MDMT Calcs; Thickness ratio per UCS-66(b)(1)(-b).
[ 6] - MDMT Calculations at the Shell/Head Joint.
[ 7] - MDMT Calculations for the Straight Flange.
[ 8] - Cylinder/Cone/Flange Junction MDMT.
[ 9] - Calculations in the Spherical Portion of the Head.
[10] - Calculations in the Knuckle Portion of the Head.
[11] - Calculated (Body Flange) Flange MDMT.
[12] - Calculated Flat Head MDMT per UCS-66.3
[13] - Tubesheet MDMT, shell side, if applicable
[14] - Tubesheet MDMT, tube side, if applicable
[15] - Nozzle Material
[16] - Shell or Head Material
[17] - Impact Testing required
[18] - Impact Testing not required, see UCS-66(b)(3)
[19] - Select a valid hydrotest type to get the UG-20(f) exemption
[20] - Cylinder/Cone Junction MDMT based on Longitudinal Stress considerations
[21] - Bolting Material
UG-84(b)(2) was not considered.
UCS-66(g) was not considered.
UCS-66(i) was not considered.
Notes:
Impact test temps were not entered in and not considered in the analysis.
UCS-66(i) applies to impact tested materials not by specification and
UCS-66(g) applies to materials impact tested per UG-84.1 General Note (c).
The Basic MDMT includes the (30F) PWHT credit if applicable.
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°C
°C
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Vessel Design Summary:
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ASME Code, Section VIII Division 1, 2017
Diameter Spec : 1670.000 mm ID
Vessel Design Length, Tangent to Tangent
7500.00
mm
0.00
mm
Internal Design Temperature
Internal Design Pressure
93
0.690
°C
MPa
External Design Temperature
External Design Pressure
93
0.103
°C
MPa
Maximum Allowable Working Pressure
External Max. Allowable Working Pressure
Hydrostatic Test Pressure
6.265
2.464
0.000
MPa
MPa
MPa
0.0
11.0
°C
°C
Specified Datum Line Distance
Required Minimum Design Metal Temperature
Warmest Computed Minimum Design Metal Temperature
Warning: Computed overall MDMT was higher than the required value !
Wind Design Code
Earthquake Design Code
UBC
UBC-97
Materials of Construction:
Component
Type
Material
Class
Shell
Hrz Bolting
SA-516 70
SA-193 B7
...
...
2 1/2
Thickness
UNS #
Normal
ized
Impact
Tested
...
<= 4
K02700
G41400
No
No
No
No
<
t
Normalized is determined based on the UCS-66 material curve selection and Figure UCS-66.
Impact Tested is based on material selection and material data properties.
Element Pressures and MAWP (MPa & mm):
Element Description
or Type
Design
Pressure
+ Stat. head
Ext.
Press.
Element
M.A.W.P
Corrosion
Allowance
Str.
Flg.
Gov.
In
Creep
Range
Cylinder
0.690
0.10
6.265
0.0000
N/A
No
Nominal
Thickness
mm
Finished
Thickness
mm
Reqd Thk
Internal
mm
Reqd Thk
External
mm
Long
Eff
Circ
Eff
...
39.0
4.2
10.3
1.00
1.00
Element Types and Properties:
Element
"To" Elev
Type
mm
Element
Length
mm
Cylinder
7500.0
7500.0
Saddle Parameters:
Saddle Width
Saddle Bearing Angle
Centerline Dimension
Wear Pad Width
Wear Pad Thickness
Wear Pad Bearing Angle
Distance from Saddle to Tangent
300.000
120.000
1174.000
350.000
10.000
132.000
470.000
mm
deg.
mm
mm
mm
deg.
mm
Baseplate Length
Baseplate Thickness
1900.000
26.000
mm
mm
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Baseplate Width
Number of Ribs (including outside ribs)
Rib Thickness
Web Thickness
Height of Center Web
Page 30 of 30
Oct 21,2019
300.000
4
10.000
10.000
306.000
mm
mm
mm
mm
Baseplate Sketch
|------------------- 1900.000 mm --------------------|
------------------------------------------------------ --|
|
|
| 300.000 mm
|
|
------------------------------------------------------ --Baseplate Plan View
------------------------------------------------------ --|
| 26.000 mm
------------------------------------------------------ --Baseplate Side View
Summary of Maximum Saddle Loads, Operating Case :
Maximum Vertical Saddle Load
Maximum Transverse Saddle Shear Load
Maximum Longitudinal Saddle Shear Load
Summary of Maximum Saddle Loads, Operating Case, Un-Factored :
Maximum Vertical Saddle Load
Maximum Transverse Saddle Shear Load
Maximum Longitudinal Saddle Shear Load
Weights:
Fabricated
Shop Test
Shipping
Erected
Empty
Operating
Field Test
-
Bare W/O Removable Internals
Fabricated + Water ( Full )
Fab. + Rem. Intls.+ Shipping App.
Fab. + Rem. Intls.+ Insul. (etc)
Fab. + Intls. + Details + Wghts.
Empty + Operating Liquid (No CA)
Empty Weight + Water (Full)
94863.10
14061.12
28122.25
N
N
N
107818.91
32344.21
39386.91
N
N
N
12751.2
29172.0
12751.2
12751.2
12751.2
12751.2
29172.0
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kgm
kgm
kgm
kgm
kgm
kgm
kgm