Validation of a Power Transformer Model for Ferroresonance with System Tests on a 400 kV Circuit Charalambos Charalambous1, Z.D. Wang1, Jie Li1, Mark Osborne2 and Paul Jarman2 Abstract-- National Grid has performed in the past a number of switching tests on a circuit configuration which was known to exhibit ferroresonance. The aim of the tests was to establish the likelihood of ferroresonance and quantify the effect on switchgear due to the de-energisation of a power transformer attached to a long over head line circuit. This paper, describes and compares the modeling work carried out in ATP (commercially available software) with the field ferroresonance test recordings. The accomplishment of a suitable simulation model will allow sensitivity studies to be carried out to determine the degree of influence of different components and parameters on the ferroresonance phenomenon. Keywords: ATP, Ferroresonance, Simulation Model, Field Tests. Power Transformer, I. INTRODUCTION Certain Failing to detect or remove a ferroresonant condition can result in overheating of parts of the transformer as it is being repeatedly driven into magnetic saturation by the ferroresonance. Both instrument transformers and power transformers can be subject to ferroresonance. In 1998 National Grid performed a number of switching tests on a circuit configuration which was known to exhibit ferroresonance. This paper describes the modeling work carried out in ATP [2] (commercially available software) to reproduce the field ferroresonance tests performed. Furthermore, the accomplishment of a suitable simulation model will allow the authors to perform sensitivity studies to determine the degree of influence of different components and parameters on the ferroresonance phenomenon [3]. circuit configuration of the UK transmission network provides an ideal environment for ferroresonance to occur. The possibility of Ferroresonance can be eliminated by the use of additional circuit brakers; however the economic justification needs to be carefully considered. Ferroresonance can be established when a transformer feeder circuit has been isolated, but continues to be energized through capacitive coupling to the energized parallel circuit [1]. A particular example is when one side of a double circuit transmission line connected to a transformer is switched out but remains capacitively energized, normally at a subharmonic frequency, because of coupling from the parallel circuit. Recovering from this condition requires the operation of a disconnector or earth switch on the resonating circuit, potentially resulting in arcing and damage, or switching off the parallel circuit resulting in an unplanned double circuit outage. II. THE 400KV DOUBLE CIRCUIT CONFIGURATION A. Physical Circuit Description and Testing The Brinsworth/ Thorpe Marsh circuit was identified as a suitable circuit that could be induced to resonate, and that could be reasonably accessed. The purpose of the tests was to establish the likelihood of ferroresonance to occurring and the impact on the switchgear during quenching of the condition. [4]. Figure 1 illustrates a single line diagram of the Brinsworth/ Thorpe Marsh circuit arrangement. The length of the parallel overhead line circuit is approximately 37km and the feeder has a 1000 MVA 400/275/13 kV power transformer. SGT1 X303 OPEN X103 CLOSED X113 CLOSED T10 OPEN Cable 170 m X420 POW switching Mesh Corner 3 Thorpe Marsh 400 kV 1. Charalambos Charalambous Zhongdong Wang and Jie Li are with the School of Electrical and Electronic Engineering, The University of Manchester, Manchester, M60 1QD, U.K (charalambos.charalambous@manchester.ac.uk, zhongdong.wang@manchester.ac.uk). 2. Mark Osborne and Paul Jarman are with National Grid, UK (mark.osborne@uk.ngrid.com, paul.jarman@uk.ngrid.com). Presented at the International Conference on Power Systems Transients (IPST’07) in Lyon, France on June 4-7, 2007 Cable 170 m SGT2 Brinsworth 275 kV Fig. 1. Single line diagram of the Brinsworth / Thorpe Marsh circuit arrangement It should be noted this is not a normal running arrangement, however to facilitate the testing this configuration was used on the day. The circuit equipment conditions prior to Ferroresonance testing are as follows: At Thorpe Marsh 400 kV substation side the disconnector X303 was locked open and mesh corner 3 restored to service. At Brinsworth 275kV substation the circuit breaker T10 is open. At Brinsworth 400kV substation all disconnectors and circuit breaker X420 are in service. Point-on-wave (POW) switching was carried out on the Brinsworth/ Thorpe Marsh circuit using circuit breaker X420 to induce Ferroresonance. This type of switching prevents switching overvoltage conditions and provides a degree of controllability to the tests. The circuit breaker was tripped via an external POW control device. data available and is illustrated by Table I. For cylindrical coil construction, it is assumed that the flux in the winding closest to the core will mostly go through the core, since there should be very little leakage. This winding is usually the tertiary winding, and is therefore best to connect the nonlinear inductance across the tertiary terminals. Although attaching the non-linear effect externally is an approximation, it is reasonably accurate for frequencies below 1 kHz [5]. TABLE I TRANSFORMER MAGNETIZING CHARACTERISTICS Current (A) Flux Linkage (Wb-turn) 7.18 48.77 7.85 52.02 8.35 55.27 19.37 58.52 35.40 61.77 78.48 65.02 222.09 65.92 5531.04 66.72 After each switching operation the POW switching control was advanced by 1ms. At +3ms POW switching, a subharmonic mode ferroresonance was established, while at +11ms POW a fundamental mode ferroresonance was induced. The ferroresonance voltage and current waveforms available from field tests are illustrated in Appendix I .The waveforms presented correspond to the fundamental and subharmonic case. B. Simulation Model Description An ATP model has been developed to simulate the testing carried out on the circuit with the ultimate purpose to match field recordings that were available. Figure 2 illustrates a layout of the simulation model, which includes a description of the components of the model. The main components of the network are: a parallel overhead line circuit (37 km) modeled considering the transmission line characteristics (typical overhead line spacings for a 400kV double circuit) [7], a transformer model utilizing the BCTRAN transformer matrix mode. Saturation effects have been considered by attaching the non- linear characteristics externally in the form of a non-linear inductive element branch. ATP Draw Model 6.3 m 9.12 m 9.12 m 7.12 m 7.12 m Series and Shunt capacitances of windings 40.5m 30.8m TV BUS A 21.5m TV BUSB C. Transformer Characteristics and Data The transformer characteristics available are tabulated in Table II. TABLE II TRANSFORMER CHARACTERISTICS Rating Type Core Construction Vector Bolt main: Bolt Yoke: % Ratio 4&5 \ Y \ M Transformer nonlinear characteristics 6.3 m In low frequency transformer models is possible to represent each winding as one element. This does not come at the expense of accuracy. The model also comprises the interwinding and shunt capacitance elements, which have been calculated by employing mathematical methods taking into consideration the transformer equivalent circuit and the winding disc configurations types. 1000 MVA 400/275/13 kV (auto) Five Limb Core Yy0 No No 60\60\100 12.8m TV BUSC TV-LV A TV-LV B TV-LV C X103 U X303 X113 LV BUSA LV BUSB LV BUSC Circuit Breaker Committee type disconnectors T 10 BCTRAN model 37km Cable 170m HV-LV A HV BUSC U HV BUSB HV BUSA HV-LV B COWL Circuit Breaker X420 POW The transformer has been modeled in the BCTRAN module of ATP draw which utilizes an admittance matrix representation of the form (1) [ I ] = [Y ].[V ] HV-LV C and in transient calculations can be represented as SGT 2 Fig. 2. Layout of ATPDraw simulation Model, including a description of the components characteristics utilized Non-linear inductances can be modeled as a two slope piecewise linear inductances, with sufficient accuracy [2]. The slope in the saturated region above the knee reflects the air core inductance which is almost linear and low compared with the slope in the unsaturated region. The transformer magnetisation curve has been derived from manufacturer’s [ di ] = [ L] −1 [v] − [ L] −1 ⋅ [ R ][i ] dt (2) The elements of the matrices are derived from open circuit and short circuit tests that are made in the factory. The data used in this simulation model include impedances and losses averaged for the test results of 8 transformers rated at1000 MVA (400/275/13 kV). Saturation effects have been modeled externally as previously described. The impedances and load losses can only be measured for winding pairs, but the designed load capability for the tertiary winding of this 1000 MVA design is only 60 MVA compared with the 1000 MVA throughput for the HV and LV terminals. Thus the H-T and L-T losses and impedances would be measured at 60 MVA. For this simulation model data a common base load is chosen to be 1000 MVA. In service, the tertiary load would never be above 60 MVA if it was loaded, so the total losses for three-winding loading would be not much greater than the H-L load loss at 1000 MVA. The impedances and losses averaged for the test results of 8 transformers are tabulated in Table III. TABLE III point has been marked as a reference point to start POW switching. Fundamental and subharmonic ferroresonance waveforms have been produced by simulation at a specific time. Table IV illustrates a comparison between the POW switching time corresponding to the field tests and to the simulation model. The ferroresonance voltage and current waveforms produced by simulation are also illustrated in Appendix I. TABLE IV P.O.W SWITCHING TIME COMPARISON Field Waveform Simulation Tests Description POW switching Impedance (%) Power (MVA) Loss (kW) HV-LV 15.8 1000 1764 HV-TV 117.2 1000 (60) 28677 (1720.62) LV-TV 91.5 1000 (60) 29875 (1792.5) Furthermore, the average no-load loss at rated voltage and frequency (measured on the tertiary) was 74.4 kW, whilst the average magnetizing current was 0.012% at 1000 MVA base. Zero sequence data was not available and therefore zero sequence data that had been employed in this simulation model has been set equal to the positive sequence data. This is a reasonable assumption to make for a 5-limb core transformer with a tertiary winding. Provision of a tertiary winding on 5limb cores drastically alters the zero sequence impedance, since zero sequence currents are able to circulate around the delta tertiary winding and thus balance those flowing into the primary winding [6]. Without a tertiary winding, the 5 limb core would have a higher zero sequence impedance (than the case where a tertiary winding is present) due to the 4th and 5th return limbs shunting the high reluctance zero sequence path (air path). The 4th and 5th return limbs of a 5 limb core are of much reduced section compared with the three main limbs. A zero sequence test at full load current would cause the 4th and 5th limbs to saturate and the core would turn into a 3-limb equivalent. In such a case the assumption of setting the zero sequence equal to the positive sequence data would not be valid. +3 ms +3.2 ms Subharmonic Mode +11 ms +12.6 ms Fundamental Mode control (time) POW switching control (time) The following set of figures illustrates a comparison of a sector of the final steady state ferroresonance mode waveforms produced by ATP and those available from field recordings, for the fundamental and subharmonic case, for each one of the 3 phases (R, Y, and B). Figures 4-9 compare the simulation results with the field results obtained for voltage and current corresponding to Phase R, Y and B respectively, for the fundamental mode ferroresonance. 300 250 200 150 Voltage Magnitude (kV) TRANSFORMER SHORT CIRCUIT FACTORY DATA 100 50 0 -50 -100 -150 -200 -250 2 2.05 2.1 2.15 2.2 Time (s) Simulation Results_Phase R Field Test Results_Phase R Fig. 4. Comparison of Fundamental Mode Ferroresonance- Section of Voltage waveform – R phase 250 200 150 100 ATP MODEL VERIFICATION Current (A) 50 III. 0 -50 The circuit conditions described in section A of II, in terms of the disconnectors and circuit breakers status, were considered in the simulation model. Circuit breaker X420, was utilized to carry out POW switching to initiate ferroresonance. -100 -150 -200 -250 2 2.05 2.1 2.15 2.2 Time (s) Simulation Results It should be noted that the circuit breaker X420 was tripped at a point in time (simultaneously for the three phases) that would ensure minimum voltages and energy transfer. This Field Test Results Fig. 5. Comparison of Fundamental Mode Ferroresonance- Section of Current waveform – R phase Figures 10-15 compare the simulation results with the field results obtained for voltage and current corresponding to phase R, Y and B respectively, for the subharmonic mode ferroresonance. 400 300 Voltage Magnitude (kV) 200 100 120 0 100 -100 80 60 Voltage R-Phase (kV) -200 -300 -400 2 2.05 2.1 2.15 2.2 Time (s) Simulation Results_Phase Y 40 20 0 -20 Field Test Results_Phase Y -40 Fig. 6. Comparison of Fundamental Mode Ferroresonance- Section of Voltage waveform – Y phase 300 -60 -80 -100 1.6 1.65 1.7 1.75 1.8 1.85 1.9 1.95 Time (s) Field Test Results 200 Fig. 10. Comparison of subharmonic Mode Ferroresonance- Section of Voltage waveform – R phase 100 Current (A) Simulation Results 50 0 40 -100 30 20 Current R phase (A) -200 -300 2 2.05 2.1 2.15 2.2 Time (s) Simulation Results 10 0 -10 Field Test Results -20 Fig. 7. Comparison of Fundamental Mode Ferroresonance- Section of Current waveform – Y phase -30 -40 -50 1.6 1.65 1.7 1.75 1.8 1.85 1.9 1.95 Time (s) 250 Field Test Results Simulation Results 200 Fig. 11. Comparison of subharmonic Mode Ferroresonance- Section of Current waveform – R phase 150 150 50 100 0 -50 50 Voltage Y phase (kV) Voltage Magnitude (kV) 100 -100 -150 -200 0 -50 -250 2 2.05 2.1 2.15 2.2 -100 Time (s) Simulation Results Field Test Results -150 Fig. 8. Comparison of Fundamental Mode Ferroresonance- Section of Voltage waveform – B phase 250 1.6 1.7 1.75 1.8 1.85 1.9 1.95 Time (s) Field Test Results Simulation Results Fig. 12. Comparison of subharmonic Mode Ferroresonance- Section of Voltage waveform – Y phase 200 150 80 100 60 50 40 0 Current Y Phase (A) Current (A) 1.65 -50 -100 20 0 -20 -150 -40 -200 -60 -250 2 2.05 2.1 2.15 2.2 -80 Time (s) Simulation Results Field Test Results 1.6 1.65 1.7 1.75 1.8 1.85 1.9 1.95 Time (s) Fig. 9. Comparison of Fundamental Mode Ferroresonance- Section of Current waveform – B phase Field Test Results Simulation Results Fig. 13. Comparison of subharmonic Mode Ferroresonance- Section of Current waveform – Y phase 100 TABLE VI COMPARISON OF FIELD AND SIMULATION RESULTS (SUBHARMONIC) 80 60 Field Test Results Voltage B phase (kV) 40 0 -20 Simulation Results Peak Voltage (kV) RMS Volt. (kV) Peak Voltage (kV) RMS Volt. (kV) R Phase 90 48.29 75 50.64 Y Phase 100 60 95 69.41 50 37.06 45 41.05 20 -40 B Phase -60 Field Test Results -80 1.6 1.65 1.7 1.75 1.8 1.85 1.9 1.95 Time (s) Field Tests RMS Cur. (A) Peak Current (A) RMS Cur. (A) R Phase 45 9.28 35 5.6 Y Phase 42 8.997 50 9.3 B Phase 38 8.72 35 5.5 Simulation Results Fig. 14. Comparison of subharmonic Mode Ferroresonance- Section of Voltage waveform – B phase Simulation Results Peak Current (A) -100 50 40 The minor differences on the voltage and current waveforms that appear on the illustrated Figures can also be seen on the frequency analysis waveforms illustrated by Figures 16 and 17, for the fundamental and subharmonic case respectively. Figures 16 and 17 compare the frequency content of voltage waveforms of the field recording results and the produced simulation results for one phase. 30 Current B phase (A) 20 10 0 -10 -20 -30 -40 -50 1.6 1.65 1.7 1.75 1.8 1.85 1.9 1.95 Time (s) Field Test Results Simulation Results Fig. 15. Comparison of subharmonic Mode Ferroresonance- Section of Current waveform – B phase The figures presented clearly illustrate that the ATP model can replicate the field recordings with a significant degree of accuracy, both in the fundamental and subharmonic case. For the subharmonic case the ferroresonance condition had a frequency content of 16 2/3 Hz. Table VI tabulates the peak and rms voltage and current values corresponding to field recordings and to simulation results. Fig. 16. Comparison of Frequency content of voltage waveforms (Fundamental –Y phase ) TABLE V COMPARISON OF FIELD AND SIMULATION RESULTS (FUNDAMENTAL) Field Test Results Simulation Results (B) Peak Voltage (kV) RMS Volt. (kV) Peak Voltage (kV) RMS Volt. (kV) R Phase 210 191 190 151 Y Phase 330 315 325 303 180 173 190 167 B Phase Field Test Results Simulation Results Peak Current (A) RMS Cur. (A) Peak Current (A) RMS Cur. (A) 200 62.56 145 46.45 Y Phase 220 70 220 70.52 B Phase 190 58.93 140 45.79 R Phase Fig. 17. Comparison of Frequency content of voltage waveforms (subharmonic – Y phase) IV. CONCLUSIONS For the fundamental case the ferroresonance condition had a frequency content of 50 Hz. Table V tabulates the peak and rms voltage and current values corresponding to field recordings and to simulation results. Ferroresonance is a low frequency phenomenon that can occur when a transmission line connected to a transformer is switched out with the parallel circuit still energised. The complex UK network is such that a few power transformers are exposed to ferroresonance on mesh corner and circuit tee connections, mainly because of historical design precedents. Fundamental mode ferroresonance R phase Current (A) Fundamental mode ferroresonance Y phase Current (A) Fundamental mode ferroresonance B phase Current (A) 300 200 Current (A) 100 0 -100 -200 -300 1500 1550 1600 1650 1700 1750 1800 1850 1900 1950 2000 Time (ms) Fig. 19. Fundamental Mode Ferroresonance – Current (Field Recordings) Sub-harmonic mode ferroresonance R phase Voltage (kV) Sub-harmonic mode ferroresonance Y phase Voltage (kV) Sub-harmonic mode ferroresonance B phase Voltage (kV) 200 150 Voltage (kV) 100 50 0 -50 -100 -150 -200 1200 1300 1400 1500 1600 1700 1800 1900 Time (ms) Fig. 20. Subharmonic Mode Ferroresonance – Voltage (Field Recordings) Sub-harmonic mode ferroresonance R phase Current (A) Sub-harmonic mode ferroresonance Y phase Current (A) Sub-harmonic mode ferroresonance B phase Current (A) 100 80 60 40 20 0 -20 -40 Current (A) A reliable ATP based simulation model can be achieved when the parameters of the system and transformer are known or can be derived with reasonable accuracy. The graphical results presented in this paper clearly demonstrate the capability of the simulation model to reproduce the field recordings with a significant degree of accuracy, both in the fundamental and subharmonic case. The development and validation of this simulation model with the field recordings available allowed the authors to perform a number of sensitivity studies that deal with the effect on ferroresonance of point on wave (P.O.W) switching, transmission line and core losses and the interaction between these variables. The sensitivity studies investigate the effect the above described interactions have on energy transfer in the transformer, on the magnitude of ferroresonant voltages and currents and the duration of overvoltages, etc. The findings are the topic of a scientific paper submitted [3]. Lastly this simulation model will form the benchmark and will produce the input data of a detailed (topologically and geometrically accurate) transformer model that would enable the understanding of magnetic field analysis (heating and fluxing) within a transformer under ferroresonance and its degrading mechanisms. -60 -80 -100 1200 1300 1400 1500 1600 1700 1800 1900 Time (ms) Fig. 21. Subharmonic Mode Ferroresonance – Current (Field Recordings) B_Phase Voltage Y_Phase Voltage R_Phase Voltage 600 The authors gratefully acknowledge the EPSRC – RAIS funding scheme and National Grid for the financial support. The authors also acknowledge the technical support provided by National Grid. Voltage (kV) 400 V. ACKNOWLEDGEMENT -600 2.5 [3] [4] [5] [6] [7] 2.65 2.7 2.75 2.8 2.85 2.9 2.95 3 Fig. 22. Fundamental Mode Ferroresonance – Voltage (Simulation Results) R_Phase Current Y_Phase Current B_Phase Current Current (A) 200 100 0 -100 -200 -300 2.5 2.55 2.6 2.65 2.7 R_Phase Voltage 2.9 2.95 3 Y_Phase Voltage B_Phase Voltage 150 100 50 0 -50 -100 -150 -200 2.5 2.6 2.7 2.8 2.9 3 3.1 3.2 3.3 3.4 3.5 Time (s) Fig. 24. Subharmonic Mode Ferroresonance – Voltage (Simulation Results) Current (A) 0 -100 -200 -300 2.85 200 Fundamental mode ferroresonance R phase Voltage (kV) Fundamental mode ferroresonance Y phase Voltage (kV) Fundamental mode ferroresonance B phase Voltage (kV) 300 200 100 2.8 Fig. 23. Fundamental Mode Ferroresonance – Current (Simulation Results) R_Phase Current 500 400 2.75 Time (s) VII. APPENDIX Voltage (kV) 2.6 300 National Grid Seven Year statement ‘Control of Ferroresonance’ Technical Guidance Note, December 2004, National Grid, UK, www.nationalgrid.com/sys ATP Rule Book and Theory Book, Can/Am EMTP User Group, Portland, OR, USA, 1997. C. Charalambous, ZD Wang, Mark Osborne, Paul Jarman, ‘’ Sensitivity studies on a power transformer model for ferroresonance on a 400 kV Circuit. IET Proceedings in Generation, Transmission and Distribution (Under Review) ‘Ferroresonance Tests on Brinsworth-Thorpe Marsh 400 kV circuit’, Technical Report TR (E) 389, Issue 1, July 2001, National Grid, UK.. Juan A. Martine-Velasco, Bruce A. Mork, ‘’Transformer Modeling for Low Frequency Transients – The state of the Art, IPST 2003 New Orleans, USA. A.C Franklin, D.P Franklin, The J&P Transformer Book, 12th Revised edition , Elsevier Science & Technology British Electricity International, Modern Power Station Practice, EHV Transmission, Volume K, Pergamon Press -400 -500 1500 2.55 Time (s) Voltage (kV) [2] 0 -200 -400 VI. REFERENCES [1] 200 Y_Phase Current B_Phase Current 100 80 60 40 20 0 -20 -40 -60 -80 -100 2.5 2.6 2.7 2.8 2.9 3 3.1 3.2 3.3 3.4 3.5 Time (s) 1550 1600 1650 1700 1750 1800 1850 1900 1950 2000 Time (ms) Fig. 18. Fundamental Mode Ferroresonance – Voltage (Field Recordings) Fig. 25. Subharmonic Mode Ferroresonance – Current (Simulation Results)