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Frequency domain transient analysis of electrical
networks including non-linear conditions
Pablo Morenoa,*, Pablo Gomeza, Jose L. Naredoa, J.L. Guardadob
aCentro de Investigacion y de Estudios Avanzados del IPN, A.P. 31-438, Plaza la Luna, 44550 Guadalajara, Jal., MexicobInstituto Tecnologico de Morelia, A.P. 262, Morelia, Mich., Mexico
Received 4 April 2003; revised 11 August 2004; accepted 24 September 2004
Abstract
This paper describes a method for the analysis of electromagnetic transients in multiphase transmission networks using the Numerical
Laplace Transform. The proposed procedure is based on the superposition principle and is applied to switching and non-linear elements
modeling. Switching operations are modeled as initial condition problems by means of injected current sources. In the case of non-linear
elements, a piece-wise linear approximation is made, which reduces the problem to a sequence of switching operations. Several applications
and comparisons with results obtained with the EMTDC and ATP programs are presented.
q 2004 Elsevier Ltd. All rights reserved.
Keywords: Electromagnetic transient analysis; Numerical Laplace transform; Nonlinearities; Power system transients; Switching transients
1. Introduction
Transient overvoltages are commonly caused by energiza-
tion or reclosure of transmission lines, as well as by faults
occurrence and clearance. Time domain methods represent the
current trend of modeling for electromagnetic transient
analysis. These methods possess great versatility simulating
sequential changes of electrical networks topology and non-
linear elements. Among time domain methods the approach
introduced by Dommel [1] is nowadays the most powerful
existing tool for transient analysis in power systems. As an
inherent nature of time domain methods dealing with elements
with frequency dependent parameters introduces complicated
convolution procedures. Although these methods have
recently incorporated frequency dependent representations
of overhead lines and cables, these procedures have not been
extensively tested [2]. On the other hand, when using
frequency domain techniques to analyze electromagnetic
transients, the frequency dependence of the electrical
0142-0615/$ - see front matter q 2004 Elsevier Ltd. All rights reserved.
doi:10.1016/j.ijepes.2004.09.003
* Corresponding author. Tel.: C52 33 3134 5570; fax: C52 33 3134
5579.
E-mail address: [email protected] (P. Moreno).
parameters can be taken into account very easily [3,4].
In spite of the fact that this later technique has been well
established for several years, a computer program of general
access is still missing. One problem here has been that dealing
with changes in network topology and with non-linear
elements presents some difficulties.
In order to develop a frequency domain method able to
solve practical problems, the superposition principle can be
used [4,5]. When applying this principle, discontinuities
(i.e. switch maneuvers) are treated as initial conditions
problems and non-linear elements (i.e. surge arresters) are
reduced to a series of sequential discontinuities. The general
procedure consists of adding the response due to certain
initial conditions to that due to the injection of some voltage
or current source.
In this paper, a technique for modeling switches and non-
linear resistors when using the numerical Laplace transform
method (NLT) is proposed. Numerical inversion of the
Laplace transform produces errors due to truncation of
integration range and discretization of the frequency
spectrum [6]. Practical insight on reducing these errors is
also presented. Three application examples are used for
testing the method and comparisons with EMTDC and ATP
results are provided.
Electrical Power and Energy Systems 27 (2005) 139–146
www.elsevier.com/locate/ijepes
P. Moreno et al. / Electrical Power and Energy Systems 27 (2005) 139–146140
2. Frequency response of a network
In this work, the nodal analysis method is adopted to deal
with transmission networks. The bus admittance matrix is
built from the admittance representation of the network’s
elements. In the case of multiphase transmission lines the
two-port admittance model is described by the following
equation
I0
Il
" #Z
Y0ðsÞcothðjðsÞlÞ KY0ðsÞcschðjðsÞlÞ
KY0ðsÞcschðjðsÞlÞ Y0ðsÞcothðjðsÞlÞ
" #V0
Vl
" #
(1)
where sZcCju; u is the angular frequency and c is a real
finite constant with a value greater or equal to zero; l is the
line length and I0, V0 are the sending end nodal current and
voltage vectors; Il, Vl are the receiving end nodal current
and voltage vectors
jðsÞ Z Mffiffiffil
pMK1 Z voltage propagation matrix (1a)
M, l are the eigenvector and eigenvalue matrices of
Z(s)Y(s)
Y0ðsÞ Z ZðsÞK1jðsÞ Z characteristic admittance (1b)
Z(s), Y(s) are per unit length impedance and admittance
matrices.
With the admittance models of all the elements of the
network, the total admittance matrix in the Laplace domain
can be formed
I1ðsÞ
«
IjðsÞ
«
INðsÞ
266666664
377777775
Z
Y11ðsÞ . YijðsÞ . Y1NðsÞ
« 1 « 1 «
Yj1ðsÞ . YjjðsÞ . YjNðsÞ
« 1 « 1 «
YN1ðsÞ / YNjðsÞ . YNNðsÞ
266666664
377777775
V1ðsÞ
«
VjðsÞ
«
VNðsÞ
266666664
377777775
(2a)
or in reduced form
IðsÞ Z YbusðsÞVðsÞ (2b)
where V(s) is the nodal voltage vector and I(s) the injected
current vector.
Expression (2a) must be solved to get the node voltages
in the Laplace domain and the waveforms in the time
domain can be obtained using the inverse Laplace trans-
form:
vðtÞ Z1
2pj
ðcCjN
cKjNVðsÞest ds (3a)
The corresponding direct Laplace transform is given by
VðsÞ Z
ðN
0vðtÞeKst ds (3b)
For practical cases (2a) cannot be solved analytically,
even for small networks. Thus, (3a) and (3b) have to be
evaluated numerically. Numerical evaluation of these
equations gives rise to truncation and discretization errors.
Practical techniques for reducing numerical errors when
inverting from the Laplace domain to the time domain are
addressed in Section 3.
3. Numerical Laplace transform
3.1. Numerical algorithm
Let v(t) be a real and causal function of time and V(s) its
image in the Laplace domain. Considering a finite
integration range, the inverse Laplace transform (3a) can
be written as
vðtÞ Z Reect
p
ðU
0Vðc C juÞejut du
� �(4a)
where U is the maximum frequency. The corresponding
direct Laplace transform is
Vðc C juÞ Z
ðT
0½vðtÞeKct�eKjut dt (4b)
where T is the observation time.
The numerical forms of Eq. (4), with odd sampling in the
frequency domain, that allow using the Fast Fourier
Transform algorithm [6] are as follows
vn Z Re Cn
XNK1
mZ0
Vm expj2pmn
N
� �( ); n Z 1; 2;.;N K1
(5a)
Vm ZXNK1
nZ0
fnDn expKj2pmn
N
� �; m Z 1; 2;.;N K1
(5b)
where
Vm Z V½c C jð2m C1ÞDu� (5c)
vn Z vðnDtÞ (5d)
Dn Z Dt expðKcnDt K jpn=NÞ (5e)
Cn Z ð2Du=pÞexpðcnDt C jpn=NÞ (5f)
Du Zp
T(5g)
Dt ZT
N(5h)
U Z2p
Dt(5i)
being Du the spectrum integration step, Dt the time
discretization step and N the number of samples.
P. Moreno et al. / Electrical Power and Energy Systems 27 (2005) 139–146 141
When performing a transient study, T is simply chosen as
the time duration of interest in the analysis. Once this has
been done the value of Du is automatically fixed according
to (5g). The time step Dt and therefore the maximum
frequency U are determined by the election on the number
of samples N, according to (5h) and (5i). A good choice of N
can be done by using the sampling theorem and considering
the maximum bandwidth required for a particular study.
Fig. 1. Errors obtained with four different windows (three cycles).
Fig. 2. Errors obtained with cZ2Du (Wilcox).
3.2. Analysis of errors
Numerical evaluation of (4a) introduces two kinds of
errors: Gibbs oscillations due to truncation of integration
range and aliasing due to discretization of the continuous
variables.
Truncation errors are reduced by introducing a ‘window’
function in the integrand of Eq. (4a). This is, V(cCju) is
multiplied by a window function s(u) and therefore it can
be written
vn Z Re Cn
XNK1
mZ0
Vmsm expj2pmn
N
� �( ); n Z 1;.;N K1
(6a)
where
sm Z ½ð2m C1ÞDu� (6b)
An evaluation of the effectiveness of four of the most
common windows, Hanning, Lanczos, Blackman and Riesz
[7], in reducing truncation errors was performed. The
window functions were applied to the numerical inversion
of the Laplace transform of a delayed cosine function
given by
f ðtÞ Z uðt KtÞcos½uðt KtÞ� (7a)
with uZ377 rad/s and tZ2 ms. The corresponding Laplace
transform of (7a) is
FðsÞ Z expðKtsÞs
s2 Cu(7b)
A number of 256 samples was used and observation
times of 1 and 3 cycles were tested. Relative errors due to
the inclusion of each window were calculated as follows
err Zf2ðtÞK f ðtÞ
max½f ðtÞ�
�������� (7c)
where f2(t) is the numerical approximation of f(t) using any
of the windows and computed according to (6a). All four
windows gave excellent results when used in one cycle.
However, as seen in Fig. 1, Lanczos and Riesz windows
gave poor results for an observation time of three cycles.
Aliasing errors can be reduced by ‘smoothing’ the
frequency response of the system. This is done by a
proper choice of the convergence factor c. Two formulas
for calculating this factor were tested. The first one was
proposed by Wilcox [6]
c Z 2Du (8a)
and the second one by Wedepohl [8]
c ZlnðN2Þ
T(8b)
The same cosine function given by (7a) was used in this
analysis. The evaluation was performed for three different
numbers of samples: 28, 210 and 212. Figures of error
obtained in this study are shown in Figs. 2 and 3. As can be
seen in Fig. 2, using the first formula provides good results,
however, the error remains almost constant when the
number of samples is varied and the observation time is
fixed to the same value. In the case of the second formula,
the error decreases as the number of samples used in the
simulation increases, as shown in Fig. 3. Therefore, with this
later formula, given the required observation time for a
particular study, aliasing errors can be reduced by increas-
ing the number of samples.
It is important to notice in Figs. 1–3, the presence of an
error of almost 100% at 2 ms. This time instant corresponds
to the cosine function delay. This is explained by the finite
elevation time that results from the numerical evaluation of
the inverse Laplace integral.
Fig. 3. Errors obtained with cZ lnðN2Þ=T (Wedepohl).
P. Moreno et al. / Electrical Power and Energy Systems 27 (2005) 139–146142
4. Switch model
Fig. 4. (a) Ideal switch and (b) practical switch model.
4.1. Ideal switch
Switching operations produce changes in network
topology that turn the network into a time variant system
precluding, apparently, the use of frequency domain
methods. However the Superposition Principle can still be
applied to overcome these problems.
An open switch can be represented by a voltage source
Vsw equal to the potential difference between its terminals.
Switch closure is accomplished by the series connection of a
voltage source Vsw2 with equal magnitude but opposite
sense to Vsw. The voltage source required to close the switch
at time tcO0 is given by
Vsw2 Z L KvswðtÞuðt K tcÞf g (9)
where vsw(t) is the time domain waveform of the voltage
between the switch terminals for the whole observation time
with the switch opened and L indicates the Laplace transform.
The total response of the electrical network is obtained
by superimposing the response due to Vsw, which is the
network operation condition existing before the switch
closure, to the response due to Vsw2.
On the other hand, a closed switch is represented by a
current source Isw, equal to the current flowing across it.
Switch opening is performed by connecting in parallel to
Isw, a current source of equal magnitude but opposite sense.
Opening the switch when the current reaches its first zero
value after a specified opening time is done by injecting a
current source Isw2 given by
Isw2 Z L KiswðtÞuðt K tzcÞf g (10)
where tzc is the current zero-crossing time and isw(t) is the
time domain waveform of the current flowing through the
closed switch for the whole observation time.
Similarly to the case of a closure the total response of the
electrical network is obtained by superimposing the
response due to Isw, to the response due to Isw2.
The current flowing through the switch, isw(t), can be
calculated employing the currents injected into one of the
switch nodes. If the switch is connected between the jth and
the kth nodes the current across it is
iswðtÞZL YjjðsÞCXn
iZ1isj
YjiðsÞ
26664
37775Vj C
Xn
iZ1isj;k
YjiðVi KVjÞ
8>>><>>>:
9>>>=>>>;
(11)
In (11), Yji is the element corresponding to the jth row and
ith column of the admittance matrix Ybus and Vj is the jth
element of the nodal voltage vector V.
4.2. Practical switch model
To deal with electrical networks the nodal analysis
method was chosen in this work. Thus ideal voltage sources
cannot be used to simulate switch closures. The injection of
voltage Vsw2 must be accomplished by means of a Norton
equivalent with current source given by
Jsw2 ZVsw2
Rx
(12)
where Rx is a resistance needed to perform the source
transformation. Rx must be small to approximate an ideal
source or it can take some particular value for representing a
contact resistance.
A practical switch model suitable for simulating closures
and openings is shown in Fig. 4. The injected current Jsw is
given by
Jsw ZVsw2
Rx
; closure
Isw2; opening
((13)
and the Norton conductance Gx is given by
Gx Z
1
Rx
; closure
K1
Rx
; opening
8>><>>: (14)
Fig. 6. Circuit for a non-linear resistance modeled with N linear segments.
P. Moreno et al. / Electrical Power and Energy Systems 27 (2005) 139–146 143
The conductance between the switch nodes must be of a
large value when it is closed or zero when it is open. This
means that a topological change of the network nodal
matrix must be done when switching occurs. Assuming
that the switch is connected between the jth and kth nodes,
modification of the nodal matrix is accomplished as
follows:
yjj / yjk
« 1 «
ykj . ykk
264
375/
yjj CGx / yjk KGx
« 1 «
ykj KGx . ykk CGx
264
375 (15)
The topological effect due to the modification represented
in (15) given the values of (14) is introducing (closure) or
extracting (opening) Rx from the network.
The complete voltage response is obtained by adding the
system response existing before switching to that resulting
from applying the current source that performs the switch
maneuver. Therefore, the complete solution corresponding
to a maneuver can be expressed as follows
V Z Vð0Þ C ðYð1ÞbusÞ
K1Ið1Þ (16)
where V(0) is the node voltages before switching, Yð1Þbus is the
admittance matrix modified according to (15) and
Ið1Þ Z½0 / Jsw / KJsw / 0�T
1 j k N(17)
5. Non-linear elements
In order to include non-linear elements in frequency
domain techniques, it is necessary to approximate the non-
linear characteristics in piece-wise linear forms. Once this
approximation has been made, the simulation procedure is
reduced to a sequence of switching operations. Fig. 5 shows
the v–i characteristic of a non-linear element approximated
by N linear segments with slopes Rn. Each segment
represents the Thevenin equivalent that the network sees
toward the non-linear element over the corresponding
operation range. The voltage between nodes j and k for
Fig. 5. Piece-wise linear approximation of a non-linear resistance.
any operation point is given by
v Z Vn CRni (18)
where Vn is the crossing point of the line with slope Rn with
the vertical axis and i is the current through the element.
The circuit that represents the piece-wise linear charac-
teristic of Fig. 5 is shown in Fig. 6. Depending on the
voltage value the branches will be connected or discon-
nected from the network using switches, as described in
Section 4. The values of Rxn and Vxn that correspond to the
Thevenin equivalent of the nth segment are given by
VXn ZRnK1Vn KVnK1Rn
RnK1 KRn
(19a)
RXn ZRnRn
RnK1 KRn
(19b)
Notice that in the simulation procedure the branches
corresponding to the linear segments have to be introduced
or extracted in a sequential order. When switch n is open
it can be closed only after switch nK1 has been closed.
On the other hand, if switch n is closed it cannot be opened
if switch nC1 is still closed. To accomplish this, the time
step Dt must be small enough to prevent jumps between
non-contiguous segments of the linear piece-wise
approximation.
6. Application examples
The proposed procedures were validated by simulating
several examples and comparing the results with those
obtained using the EMTDC and ATP programs with
frequency dependent line models. The Phase Domain Line
Model [2,9] and the J. Marti Set up [10] were used for the
EMTDC and ATP simulations, respectively. For the
frequency domain calculation, the 2-Port admittance
representation for multiphase transmission lines was
used [3,4].
Fig. 7. Circuit for example A.
Fig. 8. Conductors’ arrangement for example A.
Fig. 10. Transient recovery voltage in phase B using ATP.
P. Moreno et al. / Electrical Power and Energy Systems 27 (2005) 139–146144
6.1. Transient recovery voltage
In this example, the transient recovery voltage is
obtained when a three-phase to ground fault at the receiving
end is cleared 2 ms after line energization. The circuit and
the conductors’ arrangement are shown in Figs. 7 and 8,
respectively. Note that the system of Fig. 7 does not
represent a real case due to the pure inductance on the
source side. However, this example illustrates some
problems that can appear when using programs based on
time domain methods.
Fig. 9 shows the transient recovery voltage in phase B of
the switch obtained with the NLT program and the EMTDC.
Fig. 9. Transient recovery voltage in phase B using EMTDC and NLT.
The EMTDC-1 waveform was obtained using the same Dt
as in the NLT, while in the EMTDC-2 the Dt used was
10 times smaller. A frequency range of 0.5 Hz–0.5 MHz
was used for the vector fitting, with a maximum number of
poles/zeros of 20.
This example was also simulated using the ATP and the
results are shown in Fig. 10. The ATP-1 waveform was
found with the same Dt as the NLT, while for the ATP-2 a
Dt 10 times smaller was used. Initial frequency in the J.
Marti Setup was 0.5 Hz, considering 10 decades and 10
points/decade. The transformation matrix was computed at
5 KHz.
6.2. Surge arrester
The second application example is a sequential energiza-
tion of the line shown in Fig. 11. A surge arrester was
connected on each phase at the receiving end of the line. The
arresters were represented as non-linear resistances with v–i
Fig. 11. Circuit for example B.
Table 1
V–I characteristic of arresters
Voltage (kV) Current (kA)
480 0.176
520 0.3226
560 0.7626
600 1.6426
620 12.6426
Fig. 12. Voltage in phase B at the receiving line end.
Fig. 14. Conductors’ arrangement for example C.
P. Moreno et al. / Electrical Power and Energy Systems 27 (2005) 139–146 145
curves approximated with five linear segments whose values
are presented in Table 1. Closing times for phases A, B and
C were 3, 6 and 9 ms, respectively. Fig. 12 shows the
voltage of phase B at the receiving end. Again, the time step
of the EMTDC simulations was 10 times smaller than that of
the NLT. The same data of example A was used in the
EMTDC vector fitting routine.
Fig. 15. Voltage in phase C at the receiving node of circuit 2.
6.3. Sequential energization of a highly asymmetrical line
As a final application example, the circuit shown in
Fig. 13 is considered [11]. The conductors arrangement
consists of two flat circuits separated by a significant
distance, as shown in Fig. 14. A sequential energization of
circuit 1 was simulated, with closing times of 1.95, 3.15 and
0.25 ms for phases A, B and C, respectively. Receiving ends
of both circuits were left open.
Fig. 15 shows the voltage induced on the phase C at the
receiving node of circuit 2. In this case, the time step needed
in the EMTDC was five times larger than in the NLT to get
similar results. As can be seen in Fig. 15, there still exists a
time delay and a difference in the spikes amplitude between
the waveforms. In this case it was not possible to obtain a
better match by increasing the number of samples beyond
five times in the EMTDC.
Fig. 13. Circuit for example C.
7. Conclusions
The results obtained show the effectiveness of the
proposed method for simulating a variety of events that
generate electromagnetic transients. It was found that in
some cases the number of points needed to get correct
results using the EMTDC can be greater than that employed
by the NLT. It was also found that numerical artifacts that
produce oscillations still exist in the ATP but not in the
EMTDC. The authors’ opinion is that, although time
domain methods are more versatile than the frequency
domain ones, these last are of great help in validating the
behavior of new models for time domain programs. In
addition, the NLT simulations help to determine whether the
oscillations presented in time domain analysis are part of the
transient phenomenon or due to the numerical computations
involved.
References
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calculation of electromagnetic transients on overhead lines and
underground cables. IEEE Trans Power Deliv 1999;14(3):1032–8.
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