7i.analysis of ssr with three-level twelve-pulse vsc-based interline power-flow controller
TRANSCRIPT
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PADIYAR AND PRABHU: ANALYSIS OF SSR WITH VSC-BASED POWER-FLOW CONTROLLER 1689
both active and reactive voltage (and, hence, control of reactive
and active power) is desired. The other VSC is designated as
a support system which can inject series reactive voltageindependently [5], [7]. The capacitor voltage is regulated by dc
voltage controller of the support VSC.The dc voltage controller regulates the capacitor voltage and
maintains power balance between two converters. The power
balance can be expressed mathematically as
(1)
The independent control variables with the IPFC using two
VSCs are reactive voltage injections in two lines and active
voltage injection in prime VSC (hence, three degrees offreedom for the system shown in Fig. 1). When the active
voltage injection ofprime VSC is zero, the IPFC works sim-ilar to independent SSSCs in steady state with losses supplied
by the support VSC.
In the caseof the unified power-flow controller (UPFC), a sig-nificant increase in the damping of torsional modes is achieved
by emulating a positive resistance with the injection of seriesactive voltage [8]. A major objective of this paper is to investi-
gate the effect of active voltage injection by primeVSC of theIPFC controller on SSR damping for different operating modes.
In this paper, the interline power-flow controller (IPFC) isrealized by two three-level, 12-pulse VSCs. As there is no pub-
lished work on the analysis of SSR with IPFC, it becomes es-
sential to establish the validity of the models used. This is per-
formed by using a detailed nonlinear three-phase system model
(including the switching action within the VSC) for transient
simulation which is also used to validate the models em-ployed for the linear analysis.
The study is carried out based on eigenvalue analysis and
transient simulation. The modeling of the system neglecting
VSC is detailed (including network transients) and can be ex-
pressed in variables or (three) phase variables. The model-lingof VSC isbasedon 1) variables (neglecting harmonicsin the output voltages of the converters) and 2) phase variables
and the use of switching functions. The damping torque anal-
ysis, eigenvalue analysis, and the controller design is based on
the model while the transient simulation considers bothmodels of VSC. It is shown that series active voltage injection by
IPFC in the resistance emulation mode can effectively be used
as an SSR countermeasure.
This paper is organized as follows. The modelling of the IPFC
is described in Section II. The methods used for the analysis ofSSR are described in Section III while a case study is presented
in Section IV. Section V presents the conclusions.
II. MODELLING OF IPFC WITH THREE-LEVEL VSC
In the power circuit of an IPFC, the converter is usually
either a multipulse and/or a multilevel configuration. The con-trol of injected voltage magnitude by pulse-width modulation
(PWM) with two-level topology demands higher switching
frequency and leads to increased losses. The three-level con-
verter topology can achieve the goal by varying dead angle
with fundamental switching frequency [9]. The time period in
a cycle during which the converter pole voltage is zero is given
as [10]. The converters that allow the variation of bothmagnitude and the phase angle of converter output voltage are
Fig. 2. Equivalent circuit of a VSC viewed from the ac side.
classified as TYPE-1 converters [11]. Here, a combination of12-pulse and a three-level configuration [10] is considered. Thethree-level converter topology greatly reduces the harmonic
distortion on the ac side [5], [9]. The detailed three-phase model
of IPFC is developed by modeling the converter operation by
switching functions [10].
A. Mathematical Model in D-Q Frame of Reference
When switching functions are approximated by their fun-
damental frequency componentsneglecting harmonics, IPFCcan be modeled by transforming the three-phase voltages and
currents into variables using Krons transformation [4],[12]. The equivalent circuit of a VSC viewed from the ac side is
shown in Fig. 2.
In Fig. 2, and are the resistance and reactance
of the interfacing transformer of VSC- . The magnitude control
of the th converter output voltage is achieved by modu-
lating the conduction period affected by the dead angle of
individual converters.
The output voltage of the th converter can be represented in
the frame of reference as
(2)
(3)
(4)
where
;
for a 12-pulse converter;transformation ratio of the interfacing transformer
;angle of the th line current;
angle by which the fundamental component of
the th converter output voltage leads the th line
current . With the two converter IPFC , 2.
The dc-side capacitor is described by the dynamical equation
as
(5)
where
;
;
and components of line-1 current ;
and components of line-2 current .
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1690 IEEE TRANSACTIONS ON POWER DELIVERY, VOL. 22, NO. 3, JULY 2007
Fig. 3. IPFC controller.
B. Converter Control
Fig. 3 shows the schematic representation for converter con-
trol. In this controller, the magnitude, which is a function of
(for a constant ) and phase angle of the converter
voltage are used to control reactive and active voltage.
The support VSC regulates the dc capacitor voltage at aconstant value. The active voltage reference ofsupportVSC isobtained from the dc voltage controller while forprimeVSCs,it is obtained from constant resistance emulation. The reactive
voltage reference of support and prime VSCs can be keptconstant or obtained from the active power controller.
In Fig. 3, and are calculated as
(6)
(7)
We can define the injected reactive ( component of theinjected voltage in quadrature with line current) and the active
( component of injected voltage in phase with line current)
voltages in terms of variables in the frame ( and )as follows:
(8)
(9)
Here, positive implies that the VSC injects inductive voltage
and positive implies that it draws real power from the line.
III. ANALYSIS OF SSR
The two aspect of SSR are: 1) steady-state SSR [induction
generator effect (IGE) and torsional interaction (TI)] and 2) tran-
sient torques [4]. The analysis of steady-state SSR can be per-
formed by linearized models at the operating point and include
damping torque analysis and eigenvalue analysis. The analysis
of transient SSR requires a transient simulation of the nonlinear
model of the system. For the analysis of SSR, it is adequate to
model the transmission line by lumped resistance and induc-
tance to consider the line transients. The generator stator tran-
sients are also considered along with a detailed (2.2) model of
the generator [12]. The excitation system, including PSS, is alsoconsidered.
Fig. 4. Interaction between mechanical and electrical system.
A. Damping Torque Analysis
Damping torque analysis is a frequency-domain method
which can be used to screen the system conditions that give
rise to potential SSR problems. The significance of this ap-
proach is that it enables the planners to decide upon a suitable
countermeasure for the mitigation of the detrimental effectsof SSR. The damping torque method gives a quick check to
determine the torsional mode stability. The system is assumed
to be stable if the net damping torque at any of the torsional
mode frequencies is positive [13].
The interaction between the electrical and mechanical system
can be represented by the block diagram shown in Fig. 4.
At any given oscillation frequency of the generator rotor, the
component of electrical torque in phase with the rotor
speed is called damping torque.
The expression for the damping torque coefficient due
to the external transmission network is derived in [4] as
(10)
When the IGE is neglected (as it does not have a significant
effect on the prediction of torsional mode stability), the gener-
ator can be represented by the classical model [8].
When the mechanical damping is zero, the instability of th
torsional mode frequency is determined from the criterion
and the decrement factor can be approximately
expressed as [4], [13]
(11)
where is the modal inertia for the th mode.It is observed, generally, that the damping torque introduced
by the electrical system is at a negative peak at a frequency cor-
responding to the complement of the electrical resonance fre-
quency . The complement is defined as
(12)
where is the fundamental frequency.
B. Eigenvalue Analysis
In this analysis, generator model (2.2) [12] is considered. The
electromechanical system consists of the multimass mechan-ical system, the generator, the excitation system, power system
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1692 IEEE TRANSACTIONS ON POWER DELIVERY, VOL. 22, NO. 3, JULY 2007
TABLE I
EIGENVALUES OF THE DETAILED SYSTEM WITH AND WITHOUT IPFC
are better damped for Case 2). This results from the fact that the
loop resistance inserted by IPFC is more for Case 2). This pointis explained in some detail later. The damping of other torsional
modes (mode 2 and 3) is not significantly affected by the oper-
ating modes of IPFC.
Table I also gives the eigenvalues of the system for Case
1) when is reduced to 0.1776 (from the previous value of
0.2496) while isincreasedto 0.192 toretain the samevalue
of hybrid compensation (0.3696 p.u.) (see last column). It is ob-
served that the network resonance frequency is reduced
which increases the frequency of the subsynchronous netwok
mode to 177.16 rad/s (which does not coincide with
any of the torsional modes) and the system is found to be stable.
This suggests that it is possible to detune the network resonance
frequency by the proper selection of the combination offixed
capacitor and injected series reactive voltage for a given com-
pensation level, when the line has hybrid compensation. This is
also observed with the case studies considered for SSSC in [6],
[10], and [17].
For , it was observed that the results were not af-
fected by the absence of resistance emulation (and is held
constant). However, for being not equal to zero, there are
differences in the results as will be shown later.
It is to be noted that the injection of positive real voltage in
line-2 (positive and, hence, positive ) causes the neg-
ative real voltage injection in line-1 ( and, hence,
negative ). This is because the positive real voltage injec-tion in line-2 causes active power to be fed to line-1 from line-2
to maintain power balance in the dc link (Positive in line-2
draws real power from line-2 and supplies it to line-1 via the
dc link). Neglecting losses in the IPFC, we can express this be-
havior of IPFC from (1) as
(13)
(14)
(15)
The steady-statevariationof with obtainedby loadflow for the study system is shown in Fig. 6 for case-1. The
Fig. 6. Variation ofR
withR
.
operating points with , 0.015, 0.06, and 0.015 in per
unit are shown in Fig. 6 as A, B, C, and D, respectively.
It is to be noted from Fig. 6 that for a given change in ,
a change in is small as the current in line-1 is higher com-
pared to line-2. Hence,an increase in positive gives a small
increase in negative and the net loop resistance comprising
line-1 and 2 is increased. On the other hand, the negative re-
sistance injection in line-2 causes the net loop resistance to benegative.
Table II, column 2, gives the eigenvalues of the combined
system when series real voltage is set to 0.060 p.u. for
case-1 and the controller emulates (positive) resistance in series
with line 2 of the prime system. All of the torsional modes are
stable in this case. Comparing the results given in Tables I and II,
it is observed that the damping of mode-1 is improved with real
voltage injection, while the damping of mode-2 is marginally
reduced.
It was observed that when and the resistance
emulation is disabled, the torsional mode 1 becomes unstable
(with the eigenvalues of ). This shows that the
resistance emulation is essential, in general, to damp the criticaltorsional mode when required.
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PADIYAR AND PRABHU: ANALYSIS OF SSR WITH VSC-BASED POWER-FLOW CONTROLLER 1693
TABLE II
EIGENVALUES OF THE DETAILED SYSTEM WITH IPFC (CASE 1)AND
X = ( 0 : 2 4 9 6 + 0 : 1 2 ) = 0 : 3 6 9 6 p : u :
Fig. 7. Simulation with detailed three-phase model of IPFC for a pulse changein T ( V = 0 : 0 0 ) for Case 1).
Table II, column-3, gives the eigenvalues of the combined
system when series real voltage is set to 0.015 p.u. for
case 1 and the controller emulates negative resistance in series
with the line-2 of the prime system. It is observed that the
damping of torsional mode 2 is increased (compared to the case
with ). The damping of the subynchronous network
mode is significantly reduced in comparison with the eigenvalue
results with or 0.060. It is observed that when
, the subsynchronous network mode becomes unstable
as the net loop resistance comprising lines 1 and 2 becomeslarge negative. However, these results are not given here. In all
cases, the damping of mode-3 is practically constant as its modal
inertia is very large.
B. Transient Simulation
The transient simulation of the combined nonlinear system
with and the detailed three-phase model of the system is
carried out using MATLAB-SIMULINK [14].
The simulation results for a 10% decrease in input mechanical
torque applied at 0.5 s and removed at 1 s with case-1 (for
) using the three-phase model of IPFC is shown in
Fig. 7.
The simulation results for case-1 with the model andwith the three-phase model of IPFC are shown in Figs. 8 and
Fig. 8. Simulation with a detailedD Q model of the IPFC for a pulse change
in T ( V = 0 : 0 6 ) for Case 1).
Fig. 9. Simulation with a detailed three-phase model of the IPFC for a pulsechange in
T ( V = 0 : 0 6 )
for Case 1).
9, respectively, for 0.06. It is observed that the system
is stable (as predicted from the eigenvalue analysis). It is to be
noted that there is a good match between the simulation results
(variation of rotor angle and LPGEN section torques) ob-
tained with and three-phase models of IPFC.
C. Discussion
It was shown in [8] that the emulation of positive resistance
by the series connected VSC in a UPFC improves the damping
of the critical torsional mode. Similar results are expected in the
case of IPFC also. However, the problem is complicated by the
fact that, with IPFC connected in two parallel lines, the injec-
tion of positive series resistance in the prime line is accompa-
nied by the injection of negative resistance in the parallel line
in which support VSC is connected. Since the net resistance de-
termines the damping, it is necessary to select the prime line
with the smaller operating current such that, the loop resistance
is increased. The results of the case study prove this assertion asin example considered, the line 2 which carries about half the
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1694 IEEE TRANSACTIONS ON POWER DELIVERY, VOL. 22, NO. 3, JULY 2007
Fig. 10. Sensitivity of damping torque for variation in V .
current in line 1, is suited for the prime VSC with positive real
voltage injection. If prime VSC is connected in line 1, it must
operate with negative real voltage injection.
It was shown in [6] and [8] that the injection of constant reac-
tive voltage by series-connected VSC has no appreciable effect
on the electrical resonance frequency in the network with hybrid
compensation with fixed series capacitors. This observation canbe utilized to reduce the risk of SSR by appropriately selecting
the value of the series capacitor and making up for the required
(total) compensation by injecting constant reactive voltage. By
ensuring that the torsional mode frequency (which is unaffectedby the electrical network) does not lie close to the complement
of the electrical resonance frequency, the risk of SSR is avoided.
Although less accurate, the damping torque method can be
used to predict the potential SSR problems under various system
operating conditions. The variation of damping torque with tor-
sional frequency for case-1 is shown in Fig. 10 for various values
of . Referring to Fig. 10, peak negative damping is reduced
substantially with positive real voltage injection ,
in the line-2. However, negative real voltage injection
increases the peak negative damping. Although the peak
negative damping is decreased with positive resistance emula-
tion, the damping at higher frequencies is reduced whereas it is
increased at lower frequencies. These results are in agreementwith eigenvalue results.
Referring to (15), it should be noted that when the current of
two parallel transmission lines is nearly same, the injection of
positive active voltage in a line causes nearly equal negative real
voltage injection in the other line and there is not much increase
in the net loop resistance comprising the two lines. However, it
is possible to obtain a difference in the line currents by control
over the injected series reactive voltages. Thus, an increase of
net loop resistance of the transmission lines can be achieved and
is found to be effective in the damping of SSR. The choice of
the prime converter is based on the operating currents in the two
lines. The converter connected to the line carrying lesser current
should be operated as a prime converter with positive resistanceemulation [see (15)].
V. CONCLUSION
In this paper, we have presented the analysis and simulation
of SSR with an IPFC-compensated system which is reported for
the first time. The application of the model is validated by
the transient simulation of the three-phase model of IPFC. It
is observed that the model is quite accurate in predicting
the system performance. The effectiveness of various operatingmodes of the two VSCs comprising IPFC in damping SSR has
been investigated.
There is no appreciable difference in the resonance frequency
of the electrical network as the total series compensation (in a
hybrid compensation scheme) is increased by increasing the se-
ries reactive voltage injected instead of the series capacitor. This
reduces the risk of SSR since the fixed capacitor can be chosen
such that the electrical resonance frequency does not coincide
with the complement of the torsional modal frequency (which
is practically independent of the electrical network). This in-
dicates the possibility of detuning SSR by adjusting the series
reactive voltage wherever feasible. In addition, the injection ofseries real voltage by IPFC (to emulate positive resistance in
the transmission loop) as a SSR countermeasure is a novel tech-
nique and improves the damping of the critical torsional mode.
APPENDIX
SYSTEM DATA
The data for the electromechanical system pertaining to IEEE
SBM model [15] is based on a 600-MVA and 500-kV base. All
of the data given below are in per unit (p.u.) based on previously
mentioned base values.
IPFC controller (rating of each VSC is 100 MVA)
, .
Constant resistance emulation controller ,
.
DC voltage controller , .
The impedance of interfacing transformers is merged with the
line impedances.
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[5] N. G. Hingorani and L. Gyugyi, Understanding FACTS. Piscataway,NJ: IEEE Press, 2000.
[6] K.R. Padiyarand N.Prabhu,A comparative study of SSRcharacteris-tics of TCSC andSSSC, presentedat thePSCC Conf., Liege,Belgium,Aug. 2005.
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[9] K. K. Sen and E. J. Stacy, UPFCUnified power flow controller:Theory, modelling and applications, IEEE Trans. Power Del., vol. 13,no. 4, pp. 14531460, Oct. 1998.
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[11] C. Schauder and H. Mehta, Vector analysis and control of advancedstatic VAR compensators, Proc. Inst. Elect. Eng. C, vol. 140, no. 4,
pp. 299306, Jul. 1993.[12] K. R. Padiyar, Power System DynamicsStability and Con-trolSecond Edition. Hyderabad, India: B. S. Publications, 2002.
[13] I. M. Canay, A novel approach to the torsional interactions and elec-tricaldamping of thesynchronous machine, Part-I: Theory, Part-II: Ap-
plication to an arbitrary network, IEEE Trans. Power App. Syst., vol.PAS-101, no. 10, pp. 36303647, Oct. 1982.
[14] Using MATLAB-SIMULINK. Natick, MA: Math Works, Inc., 1999.[15] IEEE SSR working group, Second benchmark model for computer
simulation of subsynchronous resonance, IEEE Trans. Power App.Syst., vol. PAS-104, no. 5, pp. 10571066, May 1985.
[16] K. R. Padiyar and N. Prabhu, Modelling, control design and analysisof VSC based HVDC transmission systems, presented at the IEEEPOWERCON, Singapore, Nov. 2124, 2004.
[17] N. Prabhu,Analysis of subsynchronous resonance with voltage sourceconverter based FACTS and HVDC controllers, Ph.D. dissertation,Dept. Elect. Eng., Indian Inst. Sci., Bangalore, India, Sep. 2004.
K. R. Padiyar (SM91) received the B.E. degree in electrical engineering fromPoona University, Poona, India, in 1962, the M.E. degree from the Indian In-stitute of Science (I.I.Sc.), Bangalore, in 1964, and the Ph.D. degree from theUniversity of Waterloo, Waterloo, ON, Canada, in 1972.
Currently, he is an Honorary Professor of Electrical Engineering at the I.I.Sc.He was with the Indian Institute of Technology, Kanpur, India, from 1976 to1987, prior to joining I.I.Sc. His research interests are in the area of HVDC andFACTS, system dynamics, and control. He has authored three books and many
papers.Dr. Padiyar is a Fellow of the Indian National Academy of Engineering.
Nagesh Prabhu received the Dipl. Elect. Engg. degree from Karnataka Poly-technic, Mangalore, India, in 1986, the M.Tech. degree in power and energysystems from N.I.T. Karnataka, Surathkal, India (formerly Karnataka Regional
Engineering College) in 1995, and the Ph.D. degree from the Indian Institute ofScience, Bangalore, in 2005.
Currently, he is Professor of Electronics and Communication Engineering atthe VEL S.R.S. College of Multimedia (Engineering), Chennai. He was withthe N.M.A.M Institute of Technology, Nitte, from 1986 to 1998 and with J.N.N.College of Engineering, Shimoga, from 1998to 2006, prior to joining Vel S.R.S.College of Multimedia. His research interests are power system dynamics andcontrol, HVDC and FACTS, and custom power controllers.