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An Improved Power Flow for an Ill-Conditioned Power System with FACTS
Devices
NAOTO YORINO,1 TOHRU TAKEUCHI,
1 HIROSHI SASAKI,
1 and HIROAKI SUGIHARA
2
1Hiroshima University, Japan
2Chugoku Electric Power Co., Inc., Japan
SUMMARY
This paper addresses the issue of the computation
techniques for assessing the steady-state power flows con-
trolled by Flexible AC Transmission Systems (FACTS),
which contain variable series compensators (VSC), phase
shifters (PS), interphase power controllers (IPC), and
unified power flow controllers (UPFC). An improved
Newton�Raphson load flow program has been developed
based on an analysis of the convergence characteristic of
the conventional method. It is shown that the conventional
method tends to suffer from ill-conditioning problem, re-
sulting in shrinkage of the convergence region. Based on
examinations of the condition number of the Jacobian, a
penalty function method is adopted in order to avoid the
ill-conditioning problem and to guarantee a successful con-
vergence. Although the computational burden is increased
about 2 to 3 times, the proposed method considerably
extends the region of convergence. The effectiveness of the
proposed method is demonstrated through numerical ex-
aminations using IEEE 57 and 118 bus systems. © 2002
Wiley Periodicals, Inc. Electr Eng Jpn, 140(1): 30�37,
2002; Published online in Wiley InterScience (www.
interscience.wiley.com). DOI 10.1002/eej.10027
Key words: power system; power flow calculation;
ill-posed conditions; FACTS; VSC; PS; IPC; UPFC.
1. Introduction
Due to recent increases in power demand and to
power market deregulation, power transmission equipment
is being exploited more intensely; at the same time, laying
new transmission lines is difficult because of geographical,
economic, and environmental limitations. As a result, new
techniques are being developed to obtain the most carrying
capacity from existing transmission systems, while main-
taining an acceptable level of system reliability and safety.
In this context, high-performance control over power sys-
tems is necessary; in particular, techniques based on power
electronics have been attracting increasing attention [1, 2].
FACTS includes devices controlling power, voltage,
phase, impedance, and other parameters of ac networks
using power electronics. This makes it possible to improve
both the steady-state and transient characteristics as well as
the stability of power systems, while making the most of
the capacity provided by existing transmission lines, and
thus resulting in efficient and flexible networks [3]. FACTS
controllers have been increasingly employed in power sys-
tems, drawing much attention in the field of power flow
control [4�6]. In this context, a practicable efficient ap-
proach is proposed in Refs. 7 and 8 by extending the
conventional power flow calculation based on the Newton�
Raphson method to power systems equipped with FACTS
devices. The control specifications employed in conven-
tional power flow calculation (active and reactive power)
are supplemented with active line power flow (in the case
of UPFC, active line power flow and reactive line power
flow) for lines provided with FACTS devices. This ap-
proach involves finding solutions by secondary conver-
gence.
The authors have examined the approach (below
referred to as the conventional method) proposed in Refs.
7 and 8 to prove that achieving convergence is often prob-
lematical for certain FACTS devices. Thus, a new technique
offering better convergence performance is necessary. This
paper aims at clarifying the problem, and improving con-
vergence performance in power flow calculation. The
FACTS devices dealt with in this study are the VSC (Vari-
able Series Compensator), PS (Phase Shifter), IPC (Inter-
phase Power Controller), and UPFC (Unified Power Flow
Controller).
© 2002 Wiley Periodicals, Inc.
Electrical Engineering in Japan, Vol. 140, No. 1, 2002Translated from Denki Gakkai Ronbunshi, Vol. 121-B, No. 8, August 2001, pp. 967�972
30
2. The Conventional Method
The method proposed in Refs. 7 and 8 is outlined
below.
2.1 VSC (Variable Series Compensator)
The active line power flow Pkm from bus k to bus m
is expressed as
Here,
The asterisk denotes the complex conjugate.
A block diagram of the VSC is shown in Fig. 1. With
the VSC, the Pkm can be controlled by varying the line
reactance Xkm. The VSC is calculated by Newton�s method.
The correction at each iteration is found by solving the
following:
2.2 PS (Phase Shifter)
The block diagram of the PS is shown in Fig. 2. With
the PS, the Pkm can be controlled by varying the phase angle
φkm. The PS is calculated by the Newton�Raphson (N-R)
method. The correction at each iteration is found by solving
the following:
2.3 IPC (Interphase Power Controller)
A block diagram of the IPC is shown in Fig. 3. With
the IPC, the Pkm can be controlled by varying the phase
angle φkm or line reactance Xkm. The IPC can be represented
equivalently as a combination of the VSC and PS models.
When both branches are controlled via the VSC, Eq. (3) is
applied. When both branches are controlled via the PS, Eq.
(4) is applied. If one branch is controlled via the VSC and
the other via the PS, then the correction at each iteration is
found by solving the following:
Fig. 1. Variable series compensator.
(1)
(2)
(3)
(4)
Fig. 2. Phase shifter.
Fig. 3. Interphase power controller.
31
2.4 UPFC (Unified Power Flow Controller)
When the UPFC is used as a line compensator, it can
be represented by an SVS (Synchronous Voltage Source) as
shown in Fig. 4. With the UPFC, the Pkm and reactive line
power flow Qkm can be controlled by varying the magnitude
|Vs| and phase angle θs of the SVS voltage. The UPFC is
calculated by the N-R method, and the correction at each
iteration is found by solving the following:
3. Problems of the Conventional Method
In the conventional method, the N-R algorithm is
applied directly to a power system including FACTS de-
vices; here, the N-R convergence region proves to be rather
narrow for the VSC and IPC, that is, for devices that control
power flow by means of reactance. This problem was
confirmed for all systems examined (6-, 14-, 30-, 57-, and
118-bus systems) irrespective of the system scale and op-
erating conditions. On the other hand, this problem was not
detected in the case of devices that control power flow by
the phase angle, such as PS and UPFC.
For example, consider a VSC installed on line 40 of
an IEEE 57-bus system with specifications as given in Table
1. When conventional power flow control is performed by
varying the reactance Xkm of line 40 (k = 24, m = 26), the
power flow converges to Pkm < 0.24 (p.u.) as shown in Fig.
5. On the other hand, when using Pkm as a control specifi-
cation with the method proposed in Refs. 7 and 8, the
convergence limit is about Pkm < 0.16 (p.u.) as shown in Fig.
12. The mismatch in the conventional method with Pkm set
to 0.08 (p.u.) (convergence) and to 0.2 (p.u.) (divergence)
is shown in Fig. 6. Thus, with the conventional method,
convergence is not guaranteed even though a solution does
exist.
To identify the reason for this problem, the Jacobian
elements related to Pkm of the line provided with the VSC
were examined. These elements are as shown below:
Here,
(5)
Fig. 4. Unified power flow controller.
(6)
Table 1. Power control specifications (Case 1)
Line with de-
vice installed
(connected
buses)
Installed
device
FACTS
specification
(p.u.)
Before
control (for
reference)
40 (24�26) VSC Active line
power flow:
variable
0.0756
(7)
(8)
(9)
(10)
(11)
(12)
32
The above Jacobian elements were examined by repeating
the conventional power flow calculation while varying the
Xkm as a parameter (Figs. 7 and 8). As is evident from the
diagrams, all of the elements show strong nonlinear vari-
ation with respect to Xkm when Xkm is near zero. Therefore,
convergence of the N-R method cannot be expected here.
Next the condition number of the Jacobian was ex-
amined. Figure 9 shows the condition number with every
iteration when Pkm is set to 0.08 (p.u.) (convergence) and to
0.2 (p.u.) (divergence). As is evident from the diagram, the
condition number is nearly unchanged in the case of con-
vergence, while growing extremely large in the case of
divergence. In the equation
Fig. 6. Convergence characteristic of conventional
method (Case 1).
Fig. 7. Element of Jacobian (Case 1).
Fig. 8. Elements of Jacobian (Case 1).(13)
Fig. 5. Region of existence of solution for power flow
(Case 1).
Fig. 9. Number of conditions for conventional method
(Case 1).
33
it is possible that the minor noise ε included in ∆f increases
due to the enormous singular value of J�1, the original
vector ∆x0 is overridden, and the equation becomes numeri-
cally unstable. Examination of the N-R convergence proc-
ess has shown that the noise component J�1ε fluctuates
greatly.
The above discussion pertains to the VSC shown in
Fig. 1, but the same situation was also confirmed for the
VSC in the internal branch of the IPC in Fig. 3. Thus, the
above holds true for the IPC as well.
4. Improvement of Convergence Performance
(Proposed Method)
In this study, emphasis is placed on the oscillating
noise component, and the instability is removed by suppres-
sion of the oscillation. A penalty is imposed on the oscillat-
ing component to be suppressed by minimizing a penalized
function. Specifically, the penalty function p(∆x), which
increases with the oscillation of vector ∆x, is introduced,
and ∆x is chosen so as to minimize the objective function
defined as
In this study, the following quadratic form of ∆x is em-
ployed as penalty function p(∆x):
Here P is a regular symmetrical matrix. In this paper, the
unit matrix E is used for P for simplicity. In this case, Eq.
(14) may be rewritten as
The following expression is used to find ∆x so as to mini-
mize the objective function S(∆x):
Here λ is zero or positive. With greater λ, suppression of
the oscillating component provides a stronger effect but, on
the other hand, more time is required for convergence. In
this study, the parameter λ is adjusted in the following way.
1. The initial value of λ is set large enough, and the
convergence calculation is performed while suppressing the
oscillating component.
2. As the oscillating component becomes smaller, the
convergence calculation is continued at gradually de-
creased λ.
3. As the oscillating component becomes small
enough, the solution is found by the N-R algorithm as in
the conventional method.
Specifically, the initial value of λ was set to 1, and
then λ was adjusted as in Eq. (18), using the evaluation
function S(∆x) as in Eq. (16):
Once S ≤ 10�5 was reached, the solution was found
by the N-R algorithm.
Equation (18) was obtained empirically using more
than 100 random operating conditions for 6-, 14-, 20-, 57-,
and 118-bus systems. That is, Eq. (18) works for all of these
systems; on the other hand, Eq. (18) does not necessarily
provide the best convergence in all cases.
With the proposed method, Eq. (17) is solved itera-
tively using LU decomposition; however, as is evident from
the format of Eq. (17), it is very similar to the usual method
for the state estimation. Thus, since the bracketed term on
the right-hand side of Eq. (17) is a sparse matrix, the
computational burden is not dependent on system size (as
with the state estimation), but is 2 to 3 times heavier than
the conventional power flow calculation.
5. Numerical Examples
The proposed method was verified for a variety of
power systems and operating conditions, and good results
were obtained in all cases. Below, the effectiveness of the
proposed method is proved by two examples. In Case 1,
only the VSC is installed in an IEEE 57-bus system (see
Table 1) to reveal the problems with the conventional
method. In Case 2, various FACTS controllers are installed
in an IEEE 118-bus system as shown in Table 2. The authors
examined many other cases as well, while increasing the
number of FACTS devices as well as varying other parame-
ters, and stable convergence was verified in every case. For
both the proposed and conventional methods, the conver-
gence condition was set as
If the number of iterations exceeded 20, the calculation was
terminated.
5.1 Case 1
The convergence performance of the proposed
method with active line power flow set to Pkm = 0.08 (p.u.)
and Pkm = 0.2 (p.u.) is shown in Fig. 10. This convergence
pattern is typical of the proposed method. In contrast to the
conventional method, here convergence is obtained for both
settings. The variation of the number of conditions for the
(17)
(18)
(15)
(16)
(14)
(19)
34
Jacobian is presented in Fig. 11; as is evident from the
diagram, the number remains nearly unchanged.
In addition, the range of convergence was examined
by counting the number of iterations until convergence,
while varying the active line power flow as a parameter; the
results are presented in Fig. 12. The conventional method
ensured convergence with the power flow up to 0.16 p.u.;
on the other hand, the proposed method had a significantly
wider range up to 0.24 p.u. This coincides with the region
of existence of the power flow solution found by the usual
power flow calculation. Quite similar results were also
obtained for a large variety of systems.
5.2 Case 2
Here the FACTS controllers were installed as shown
in Table 2, and the comparison between the proposed and
conventional methods was made while varying the power
flow on line 16. The results are shown in Figs. 13 to 15.
Comparison shows that the proposed method (Fig. 14)
gives better convergence performance than the conven-
tional method (Fig. 13). The number of iterations until
convergence for both methods is shown in Fig. 15. As is
evident from the diagram, the proposed method achieves
convergence in a wider range, while the number of itera-
tions is nearly unchanged. Similar good results were ob-
tained for other systems.
Table 2. Power control specifications (Case 2)
Line with de-
vice installed
(connected
buses)
Installed
device
FACTS
specification (p.u.)
Before
control
(for
reference)
16 (7�12) VSC Active line power
flow: variable
0.3509
51 (33�37) IPC Active line power
flow: 0.6
0.5488
81 (55�56) PS Active line power
flow: 0.2
0.1878
140 (85�89) UPFC Active line power
flow: 0.45
0.4088
Reactive line power
flow: 0.1
0.0955
Fig. 10. Convergence characteristic of proposed method
(Case 1).
Fig. 11. Number of conditions for proposed method
(Case 1).
Fig. 12. Region of convergence (Case 1).
35
5.3 Computational burden
The computation time per iteration of the proposed
method was examined with reference to the conventional
method as unity. Figure 16 shows results for Ward & Hale
6, IEEE 14, IEEE 30, IEEE 57, and IEEE 118 power
systems, with the number of FACTS devices being 5, 10,
and 15% of the total number of lines. As stated above, the
proposed method required 2 to 3 times as much computa-
tion, irrespective of system size or the number of FACTS
controllers.
6. Conclusions
This paper has proposed a method for power flow
calculation with regard to FACTS controllers, namely,
VSC, PS, IPC, and UPFC. The proposed method gives
better convergence in a considerably wider range than the
conventional method. The computing time is 2 to 3 times
as long irrespective of system scale. The effectiveness of
the proposed method is shown by numerical examples
using IEEE 57 and IEEE 118 systems.
REFERENCES
1. Hingorani NG. High power electronics and flexible
AC transmission systems. IEEE Power Eng Review,
p 3�4, July 1988.
2. Ledu A, Tontini G, Winfield M. Which FACTS equip-
ment for which need? CIGRE 1992, Session paper
14/37/38-08.
3. Hingorani NH. Flexible AC transmission systems.
IEEE Spectrum, p 40�45, April 1993.
4. Han ZX. Phase shifter and power flow control. IEEE
Trans Power Apparatus Syst 1982;101:3790�3795.
Fig. 13. Convergence characteristic of conventional
method (Case 2).
Fig. 14. Convergence characteristics of proposed
method (Case 2).
Fig. 15. Region of convergence (Case 2).
Fig. 16. Computation time of proposed method versus
conventional method.
36
5. Noroozain M, Andersson G. Power flow control by
use of controllable series components. IEEE Trans
Power Delivery 1993;8:1420�1429.
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rithm for the control of power flow in electrical power
networks. IEEE Trans Power Syst 1997;12(4).
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AUTHORS (from left to right)
Naoto Yorino (member) completed the M.E. program at Waseda University in 1983 and joined Fuji Electric. He obtained
his D.Eng. degree from Waseda University in 1984, and joined the faculty as a research associate in 1985. He moved to Hiroshima
University in 1987, and has been an associate professor since 1991. His research interests are power system stability and
economical operation. He received the 1985 George Montefiore Award.
Tohru Takeuchi (student member) graduated from Hiroshima University (electrical engineering) in 1999 and is now a
doctoral candidate (systems engineering).
Hiroshi Sasaki (member) received his D.Eng. degree from Waseda University (electrical engineering) in 1968 and joined
the faculty of Hiroshima University as a lecturer, becoming an associate professor in 1980 and a professor in 1989. His research
interests are transient stability of power systems, state estimation, optimal flow calculation, and expert systems. He is a member
of IEEE, CIGRE, the Japan Solar Energy Society, the Information Processing Society of Japan, and the Japan Society of Energy
and Resources.
Hiroaki Sugihara (member) graduated from Kyoto University (electrical engineering) in 1981 and joined Chugoku
Electric Power Co. His research interests are power systems.
37