* Your assessment is very important for improving the workof artificial intelligence, which forms the content of this project
Download X Switching Overvoltage Mitigation Measures
Immunity-aware programming wikipedia , lookup
Three-phase electric power wikipedia , lookup
Stepper motor wikipedia , lookup
Power engineering wikipedia , lookup
Ground (electricity) wikipedia , lookup
Electromagnetic compatibility wikipedia , lookup
Power inverter wikipedia , lookup
Spark-gap transmitter wikipedia , lookup
Pulse-width modulation wikipedia , lookup
Power MOSFET wikipedia , lookup
Current source wikipedia , lookup
Electrical ballast wikipedia , lookup
Variable-frequency drive wikipedia , lookup
Power electronics wikipedia , lookup
Schmitt trigger wikipedia , lookup
History of electric power transmission wikipedia , lookup
Opto-isolator wikipedia , lookup
Alternating current wikipedia , lookup
Circuit breaker wikipedia , lookup
Voltage regulator wikipedia , lookup
Stray voltage wikipedia , lookup
Resistive opto-isolator wikipedia , lookup
Voltage optimisation wikipedia , lookup
Buck converter wikipedia , lookup
Mains electricity wikipedia , lookup
Switched-mode power supply wikipedia , lookup
X Switching Overvoltage Mitigation Measures X.1 Introduction Switching overvoltages are the primary dimensioning parameter for air-clearances on EHV and UHV systems. The reason for this is that, while clearances for lightning impulse withstand increase linearly with gap distance, those for switching impulse withstand tend to saturate with increasing gap distances (Fig. 1). Clearly, therefore, there is great merit to mitigate switching overvoltage levels. Fig. 1 Lightning and switching impulse withstand versus gap distance for rod-rod gap The historical background to this subject is interesting. The first EHV system was the 400 kV system developed in Sweden in the mid 1950s. No account was taken of switching overvoltages because their influence remained to be identified and obviously no mitigation was considered. The development of the 400 kV system in Italy in the 1960s was the first real recognition of switching overvoltages. A very large number of switching impulse tests were performed and resulted in the now well-known U-curves and the notion of gap factors [1, 2]. The explanation for the U-curve was provided by research work at EdF [3]. Switching impulse breakdown involves both streamer and leader development (lightning impulse breakdown involves streamers only) with the latter being the main driver. The minimum value of the U-curves thus represents optimal leader development and occurs at front-times in the range of 100 to 400 µs leading to a selection of a front-time of 250 µs for standardization purposes. Detailed descriptions of electrical discharges and breakdown in air can be found in [4, 5]. A number of switching overvoltage mitigation measures have been proposed or used starting in the 1960s: Fast insertion of shunt reactors [6]. Closing resistors [6, 7, 8, 9]. Staggered pole closing [10, 17, 18, 20]. Line terminal arresters [10, 11, 12, 13, 14]. Controlled closing [15, 6, 8, 16, 17, 18, 19, 20, 21]. Each of these measures will be discussed in the following sections. X.2 Fast Insertion of Shunt Reactors The primary purpose of shunt reactors is to provide compensation of transmission line capacitance and have secondary value, if connected, of providing some reduction in switching overvoltage levels. No utility would consider adding shunt reactors specifically for the latter purpose. The intent, therefore, with this proposal is to switch in disconnected reactors preferably prior to energizing or re-energizing the line [6]. Compared to other more measures discussed below, this measure is not of significant interest. 1 X.3 Closing Resistors Once the significance of switching overvoltages were introduced, closing resistors were applied on EHV airblast circuit breakers starting in the 1960s [7, 8, 9]. The principle behind the use of closing resistors is as follows. Assume a voltage UD across the open circuit breaker at the instant of closing. Closing effectively produces a travelling wave of magnitude UD which divides between the resistor R and the line surge impedance Z. The incident wave at the open end of the line is thus: UoL UD Z RZ and after voltage doubling, the line end voltage becomes UeL 2UD Z UTC RZ where UTC is the initial trapped charge on the line. Taking, for example, UD 2 (1 pu positive source voltage and 1 pu negative trapped voltage) UeL 4Z 1 RZ If R 0, then UeL 3 pu. Clearly, the higher the value of R, the lower the value of UeL. However, the resistor is inserted only momentarily and bypassing generates a travelling wave given by: UR URDR RZ where URD is the voltage across the resistor at the instant of bypassing. At the line end with voltage doubling, the voltage is: URe L 2URDR Upf RZ where Upf is the frequency voltage at the instant of travelling wave arrival. An upper limit on the value of R is therefore required. The value of R is usually optimized through computer studies and is typically in the range 250 to 600 ohms dependent on the application. Generally, the aim with closing resistors is to limit the voltage at the receiving end of the line to 2 pu. However, closing resistors do little for the voltage profile along the line and higher overvoltages than 2 pu at points where incident and reflected waves cumulatively coincide. X.4 Staggered Pole Closing Staggered pole closing is more a complimentary switching overvoltage mitigation measure than a fundamental measure [10, 17, 18, 20]. The principle is quite simply closing the individual poles one-half cycle apart in the expectation that transients in 2 the closed phase will have greatly attenuated before the next poles close. The effect is to reduce the coupling contribution in any one phase from the other two phases. This measure is inexpensive, easily implemented and reliable. X.5 Line Surge Arresters As an alterative to the use of closing resistors, metal oxide surge arresters were applied on line terminals starting in the late 1980s [10, 11, 12, 13, 14]. This has since become common practice at EHV and even at HV but there for lightning protection reasons. The effect of the line surge arresters is shown in Fig. 2 for a typical EHV application such as described in [14]. With arresters at the line ends only, the overvoltages at those points only will be limited to the protective level of the arresters. However, the voltage profile along the line shows much higher overvoltage levels and suggests a need to even out the profile. This is achieved by adding arresters at intermediate points along the line as also shown in Fig. 2. The surge arresters applied for this purpose are special in the sense that their characteristics are derived from EMTP system studies. A balance has to be achieved between the protective level and the energy absorbed which work in opposite directions, i.e. decreasing the protective level increases the energy absorbed and vice versa. In the ultimate, further reduction in the overvoltage level requires a more proactive mitigation measure. Fig. 2 Effects of line surge arresters on switching overvoltage levels X.6 Controlled Closing Controlled closing of circuit breakers to limit switching overvoltages was suggested as early as 1966 [15]; was viewed as less than practical 1969 [8]; was proposed as part of a combined closing resistor and controlled closing solution in 1970 [6]; was actually tested on a power system in 1976 [16]; but finally did not become a reality until the 1990s [17, 18, 19, 20, 21]. The reason for this delay is discussed below. When an unloaded transmission line is switched out, the remaining voltage on the line will be a DC voltage if the line is not compensated or an oscillatory voltage if the line is compensated, the frequency being dependent on the degree of compensation. The intent of controlled switching then is to close the circuit breaker when the difference between the source power frequency voltage and the line voltage is at a minimum. For the uncompensated line case, the minimum will occur once every cycle when the polarities of the source and line voltages are the same. For the compensated line case, the differential voltage minimums are frequency dependent as shown in Fig. 3. The 45 Hz case corresponds to a high degree compensation (80%) with shunt reactors at both line ends and the voltage minimums are clearly evident. At 33 Hz –low degree of compensation (40%) with shunt reactor at one end only – the minimums are less evident by comparison. 3 Traces from actual field measurements by BC Hydro are shown in Figs. 4 and 5. Fig. 5 shows that the line side oscillation is more complex than that shown in Fig. 4. In reality, three oscillation modes are involved in the 40% compensation case and the minimums become even less distinct. 2.5 60 Hz Difference 60 vs 33 Hz 2 Difference 60 vs 45 Hz 1.5 Voltage (pu) 1 0.5 0 0 20 40 60 80 100 120 140 -0.5 -1 -1.5 -2 -2.5 Time (ms) Fig. 3 Differential voltage across circuit breaker Fig. 4 500 kV line 80% compensated 4 160 180 Fig. 5 500 kV line 40% compensated It is clear that this mitigation measure requires a dynamic controller which can analyze the differential voltage across the circuit breaker, locate the minimums, predict the future minimums and close the breaker accordingly when the close signal is applied, all within 0.5 s or perhaps less. The sophistication of the control device obviously goes far beyond the zero crossing detectors and sequence timers available when this measure was first proposed. As with controlled capacitor bank switching, the rate of decay of dielectric strength (RDDS) of the circuit breaker is a factor in the application of this measure. This measure combined with line end and mid-line 372 kV rated arresters has been successfully in-service at 500 kV on the BC Hydro system since 1995 [20, 21]. The intent was to limit switching overvoltages to 1.7 pu anywhere along the line. X.7 Comparison of Various Measures Fig. 7 shows the cumulative frequency distribution for the overvoltages at the open end of a transposed 330 km long 500 kV line following high-speed reclosing for the various overvoltage limitation measures. The arresters considered were rated at 100.0 No control m easures Cumulative frequency (%) 90.0 Staggered pole closing 80.0 70.0 Closing resistors 60.0 Line term inal arresters 50.0 40.0 Line term inal plus m id-line arresters 30.0 Controlled closing plus line term inal arresters 20.0 Closing resistor 400 ohm s plus line end arresters 10.0 Closing resistor 800 ohm s plus line end arresters 0.0 1.0 1.5 2.0 2.5 3.0 Overvoltage level (pu) Fig. 6 Cumulative frequency overvoltage distributions for various overvoltage limitation options 372 kV and about an equivalent IEC Line Class 7. Clearly, staggered pole closing 5 has only incremental value and cannot be considered as stand-alone option. The value lies in the options of closing resistors, line terminal (meaning arresters at both line terminals) and mid-line arresters and controlled closing combined with line terminal arresters. The effect of the various options on the voltage profile along the line is of greater interest and this is shown in Fig. 7 for a 330 km long 500 kV line. The two options that provide the most significant line overvoltage profile limitation are closing resistors or controlled closing both combined with line terminal arresters. At 800 kV and below, closing resistors are now rarely used and either an arrester only option or the controlled closing option is adopted. At the UHV levels of 1000 kV and above, the situation is different as discussed below. 3.5 3 No control measures Overvoltgae (pu) Closing resistors (400 ohm)only Closing resistors (400 ohm) plus line terminal arresters Line terminal arresters plus SPC 2.5 Line terminal and mid-line arresters plus SPC Controlled closing and line terminal arresters Closing resistors (800 ohm) only 2 Closing resistor (800 ohm) plus line end arresters 1.5 1 0 1 2 3 4 5 6 7 8 9 10 11 12 Line Section No. Fig. 7 Overvoltage profile along 330 km long transposed 500 kV line for various overvoltage limitation options Circuit breakers applied at 1000 kV and 1200 kV will incorporate opening resistors in order to meet transient recovery voltage (TRV) requirements during fault clearing. The resistors, though probably rated resistance-wise for opening, can double as closing resistors. However, as shown in Figs. 6 and 7, the lower the resistance value the greater the overvoltage limitation value. The choice between the closing resistor versus closing controller option is a decision for the user and a comparison is given in Table 1. Table 1 Comparison of closing resistor and closing controller overvoltage limitation options Attribute Proven technology Closing resistor Yes, in use since 1960 6 Closing controller Yes, in use since early 1990s Attribute Complexity Closing resistor High; multiple moving mechanical parts Location At line potential Maintainability Low; requires circuit breaker outage Yes; parts only rather than complete module Limited if at all Provision of spares Future improvement potential Closing controller Low; no moving parts, circuit boards and associated software only At ground level in control room High; does not require circuit breaker outage Yes; complete module or circuit boards Yes, component and software advances The above discussion and study results for a transposed 500 kV transmission line illustrate the combined contribution of line end arresters and closing resistors or a controller to switching overvoltage limitation. The results can certainly be viewed as indicative of performance but, to determine absolute design parameters, the user needs to conduct studies focused on the actual application details and considerations. Accurate representation of arrester and controller characteristics, resistor insertion and line configuration is essential in order to achieve a valid design basis for lines meeting dependability requirements. References 1. G. Carrara, "Investigation on impulse sparkover characteristics of long rod/rod and rod/plane air gaps". Cigre Report No. 328, 1964. 2. L. Paris and R. Cortina, "Switching and lightning impulse characteristics of large air gaps and long insulator strings". IEEE Transactions on Power Apparatus and Systems No. 87, 1968. 3. J.N. Ross et al, "Positive discharges in long air gap at Les Renardieres." Electra No. 53. 1977. 4. N.L. Allen, "Mechanism of air breakdown." Chapter 1, Advances in High Voltage Engineering (Book), IEE Press 2004. 5. V. Cooray, "Mechanism of electrical discharges." Chapter 3, The Lightning Flash (Book), IEE Press 2003. 6. H.B. Thoren, "Reduction of Switching Overvoltages in EHV and UHV Systems." IEEE Trans. PAS-90, 1971. 7. C.L. Wagner and J.W. Bankoske, "Evaluation of Surge Suppression Resistors in High-Voltage Circuit Breakers." IEEE Trans. PAS-86, 1967. 8. P.A. Baltensperger and P. Djurdjevic, "Damping of Switching Overvoltages in EHV Networks – New Economic Aspects and Solutions." IEEE Trans. PAS-88, 1969. 9. R.G. Colclasser, C.L. Wagner and E.P. Donohue, "Multistep Resistor Control of Switching Surges." IEEE Trans. PAS-88, 1969. 7 10. A.C. Legate, J.H. Brunke, J.J. Ray and E.J. Yasuda, "Elimination of Closing Resistors on EHV Circuit Breakers." IEEE Trans. PD, Vol. 3, 1988. 11. J.R. Ribeiro and M.E. McCallum, "An Application of Metal Oxide Surge Arresters in the Elimination of Need for Closing Resistors in EHV Circuit Breakers." IEEE Trans. PD, Vol. 4, 1989. 12. J.K. Blakow and T.L. Weaver, "Switching Surge Control for the 500 kV California-Oregon Transmission Project." Cigre Report No. 13-304, 1990. 13. A. Eriksson, J. Grandl and O. Knudsen, "Optimized line switching surge control using circuit-breakers without closing resistors." Cigre Report No. 13-305. 14. Y.I. Musa, A.J.F. Keri, J.A. Halladay, A.S. Jagtiani, J.D. Manderville, B. Johnnerfelt, L. Stenstrom, A.H. Khan and W.B. Freeman, "Application of 800 kV SF6 Dead Tank Circuit Breaker with Transmission Line Surge Arrester to Control Switching Transient Overvoltages." IEEE Trans. PD, Vol. 17, 2002. 15. E. Maury, "Synchronous closing of 500 and 765 kV circuit breakers: a means of reducing switching surges on unloaded lines." Cigre Report No. 143, 1966. 16. H.E. Konkel, A.C. Legate and H.C. Ramberg, "Limiting Switching Surge Overvoltages with Conventional Power Circuit Breakers". IEEE Trans. PAS-96, 1977. 17. B. Avent and J. Sawada, "BC Hydro's Experience with Controlled Circuit Breaker Closing on a 500 kV Line." Canadian Electrical Association, Engineering and Operating Division Meeting, March 1995. 18. K. Froehlich, C. Hoelzl, A.C. Carvalho and W. Hofbauer, "Transmission Line Controlled Switching." Canadian Electrical Association, Engineering and Operating Division Meeting, March 1995. 19. A.H. Khan, D.S. Johnson, J.H. Brunke and D.L. Goldsworthy, "Synchronous Closing Application in Utility Transmission Systems." Cigre Report No. 13-306, 1996. 20. K. Froehlich, C. Hoelzl, M. Stanek, A.C. Carvalho, W. Hofbauer, P. Hoegg, B.L. Avent, D.F. Peelo and J.H. Sawada, "Controlled Closing on Shunt Reactor Compensated Transmission Lines: Part 1 Closing Control Device Development and Part 2 Application of Closing Control Device for High-Speed Autoreclosing on BC Hydro 500 kV Transmission Line." IEEE Trans. PD, Vol. 12, 1997. 21. B.L. Avent, D.F. Peelo and J. Sawada, "Application of 500 kV Circuit Breakers on Transmission Line with MOV Protected Series Capacitor Bank." Cigre Report No. 13-107, 2002. 8