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Nonlinear bearing stiffness parameter estimation in ¯exible rotor±bearingsystems using Volterra and Wiener approach
A.A. Khan*, N.S. Vyas
Department of Mechanical Engineering, Indian Institute of Technology, Kanpur, India
Accepted 14 July 2000
Abstract
Higher order frequency response functions based on Volterra and Wiener series are explored for the inverse problem of stiffness estimation
of a ¯exible rotor supported in nonlinear bearings. The Volterra series has been employed by researchers earlier for the identi®cation of
higher order kernels of nonlinear systems through a non-parametric approach. The present study investigates the possibility of employing
these kernels for parameter estimation of the system. Numerical simulation has been carried out for a system with three degrees of freedom
and with cubic nonlinearity in stiffness. A frequency domain has been adopted for the identi®cation of higher order kernels. The procedure
involves extraction of Wiener kernels from the response of the system to a Gaussian white noise excitation. Volterra kernels are in turn
synthesised from the Wiener kernels. In addition to direct kernels, the system under consideration, requires de®nitions of cross-kernels and their
estimation. Expressions for the cross and direct kernels are constructed in the frequency domain. A set of third-order kernel factors are
algebraically and graphically synthesised from the measured ®rst-order kernels. These third-order kernel factors are then processed with the
measured third-order kernels for nonlinear parameter estimation. Damping is taken to be linear in the analysis. The procedure is illustrated
through numerical simulation. The assumptions involved and the approximations are discussed. q 2001 Elsevier Science Ltd. All rights reserved.
Keywords: Rotor; Bearing; Nonlinear stiffness estimation; Volterra and Wiener series
1. Introduction
The characterisation of nonlinear dynamic systems, from
input±output data, is broadly categorised into parametric
and non-parametric identi®cations. Parametric methods
require that the mathematical structure and order of the
system are known. The identi®cation procedure, in such
cases reduces to estimation of system parameters through
a search in parameter space. Mechanical and structural
system nonlinearities, occurring in stiffness or in damping
forces are modelled generally in polynomial form. Identi®-
cation of non-polynomial forms, such as drag force type
quadratic damping, hysteretic damping, coulomb damping,
bilinear stiffness have been discussed by Nayfeh [1], Choi
et al. [2], Bendat and Piersol [3]. Bendat et al. [4] developed
a general identi®cation technique from measured input±
output stochastic data for a wide range of nonlinearities
including Duf®ng oscillator, Van-der Pol oscillator, dead
band and clearance nonlinearity. Linear system identi®ca-
tion procedure using spectral density functions were
extended by Bendat and Peirsol [5,6] for nonlinear systems,
through de®nitions of higher order spectral density
functions. Rice and Fritzpatrick [7,8] have also presented
a similar procedure. Mohammad et al. [9] presented a para-
metric method, which works directly with the differential
equation, through measurement of forcing function and
response (acceleration) at each time-step.
Non-parametric identi®cation concerns modelling in a
function space by input±output mapping, for systems
where suf®cient information on the mathematical structure
or class is not available. The input±output mapping, under
non-parametric methods, is done through a series of func-
tionals or a series of orthogonal functions. In orthogonal
series representation, such as in Restoring Force Mapping
techniques [10±14], the response variables are represented
in terms of some orthogonal series and identi®cation
attempts to determine the coef®cients of the terms in the
series. These series are generally in®nite in nature and are
to be truncated to ®nite number of terms for the purpose of
identi®cation. The restoring force mapping techniques
provide general identi®cation methods applicable for a
wide class of nonlinear systems, but the methods have the
limitation that acceleration data is integrated to give velo-
city and displacement records, which may introduce mean
bias and drift error. In the functional series representation,
Probabilistic Engineering Mechanics 16 (2001) 137±157
0266-8920/01/$ - see front matter q 2001 Elsevier Science Ltd. All rights reserved.
PII: S0266-8920(00)00016-3
www.elsevier.com/locate/probengmech
* Corresponding author.
such as in Volterra or Wiener series, the identi®cation
consists of determining the kernels of the functionals either
in the time- or frequency-domain. The Volterra series
[15,16] represents the response of a system in a functional
series form. The ®rst term in the series is the well-known
convolution integral used for input±output mapping of
linear systems. Subsequent series terms consist of higher
order convolution integral operating on the input function
through higher order impulse response function known as
Volterra kernels. Two basic dif®culties associated with
practical application of Volterra series are the convergence
of the series and the measurement of individual Volterra
kernels of the given system. These problems are circum-
vented by construction of Wiener G-functionals [17] with
Gaussian white noise excitation. Wiener kernels can be
related to Volterra kernels, using their orthogonality prop-
erty [18]. Barret [19,20] and Flake [21] have presented
various details on the use of Volterra series in nonlinear
system analysis. Schetzen [22] presented a method for
measuring the Volterra kernels as multi-dimensional
impulse responses of a ®nite order nonlinear systems. Sand-
berg and Stark [23] measured the kernels of the Pupillary
system up to second-order using Schetzen's cross-correla-
tion technique. Bedrosian and Rice [24] illustrated
frequency domain methods for response characterisation
of nonlinear systems under harmonic excitation as well as
random excitation along with effect of noise on the
measured response. French and Butz [25,26] developed a
general frequency domain method for calculation of higher
order Wiener kernels using exponential functions as a set of
orthogonal functions for expanding the kernels. Gifford and
Tomlinson [27] illustrated the technique of calculating
higher order frequency response functions (FRFs) for
nonlinear structural systems. Haber [28] has discussed the
kernel estimation of the discrete Volterra series for quad-
ratic block oriented models. Nam et al. [29] presented a
frequency domain approach for the identi®cation of a
discrete third-order Volterra system with random input.
Koukoulas and Kalouptsidis [30] proposed an approach
for identi®cation of Volterra kernels based on cross-cumu-
lants and their spectra, rather than cross-correlation.
Tomlinson et al. [31] studied the convergence of ®rst-
order FRF of a Duf®ng oscillator under harmonic excitation
and presented a simple formula for determining the upper
limit of excitation level.
In a recent study, Khan and Vyas [32] attempted to extend
the non-parametric Volterra kernel identi®cation procedure,
for further estimation of the system parameters of a single-
degree-of-freedom system. The present study discusses the
case of a more general multi-degrees-of-freedom model.
With polynomial form nonlinearity in stiffness or damping
forces, analytical expressions for higher order kernels can
be built, in terms of the ®rst-order kernel and coef®cients of
the polynomial representing the stiffness or damping forces.
These expressions are processed along with the measured
kernels for parameter estimation. The problem of conver-
gence of the Volterra series is sought to be circumvented
through estimation of Wiener kernels, under white noise
excitation. The Volterra kernels are developed, in turn,
from the Wiener kernels. The problem has been discussed
for a multi-degrees-of-freedom system, through an idealised
¯exible rotor±bearing model. Direct and cross-kernels have
been de®ned for the system and the procedure is illustrated
through numerical simulation.
2. Governing equations and Volterra series responserepresentation
The equations of motion for a balanced rotor with a
centrally located disc on a massless ¯exible shaft supported
in bearings (shown in Fig. 1) are written as
�M�{ �x} 1 �C�{ _x} 1 �K�{x} 1 �Kn�{x3} � {f �t�}
with
�M� �m1 0 0
0 m2 0
0 0 m3
26643775 �C� �
c11 c12 c13
c21 c22 c23
c31 c32 c33
26643775
�K� �k11 1 kL
b1k12 k13
k21 k22 1 kLb2
k23
k31 k32 k33
2666437775
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157138
Fig. 1. Flexible rotor in bearings.
�Kn� �kN
b10 0
0 kNb2
0
0 0 0
2666437775 {x} �
x1
x2
x3
8>><>>:9>>=>>;
{f �t�} �f1�t�f2�t�
0
8>><>>:9>>=>>; (1)
m1, m2 and m3 are the system masses at stations 1, 2 and 3,
respectively. External white noise excitation forces,
provided at the bearing stations are f1�t�; and f2�t�: kLb1
and
kLb2
are the unknown linear stiffness terms of the two bear-
ings and kNb1
and kNb2
are their unknown nonlinear stiffness
terms. The shaft stiffness kij is the resistive force at the ith
station corresponding to a unit de¯ection at the jth station,
with all other de¯ections held to zero. kij values can be
obtained from the strength of materials formulae. c11, c12,
c13, etc. are linear damping terms.
De®ning
t � pt p � ��������k33=m3
pxih�t� � xi=
iXst
iXst � Fmax=mip2 �f i�t� � fi�t�=Fmax j ij � cij=2mip
lij � kij=mip2 i; j � 1; 2; 3 lL
ij � kLbi=mip
2
lNbi� kN
biF2
max=m3i p6 for i � 1; 2 (2)
and considering only direct damping terms, to keep the
algebra simple, Eq. (1) becomes
{h 00} 1 2�j�{h 0} 1 �l�{h} 1 �lN�{h3} � { �f �t�}
�j� �j11 0 0
0 j22 0
0 0 j33
26643775
�l� �l11 1 lL
b1l12 l13
l21 l22 1 lLb2
l23
l31 l32 l33
2666437775
�lN� �lN
b10 0
0 lNb2
0
0 0 0
2666437775 {h 00} �
x1h 00
x2h 00
x3h 00
8>><>>:9>>=>>;
{ �f �t�} ��f 1�t��f 2�t�
0
8>><>>:9>>=>>;
�3�
The solution of the Eq. (3) is represented in terms of
Volterra operators as
kh�t� �X1n�1
kHn� �f 1�t�; �f 2�t�� �4�
with k denoting x1, x2 or x3. The individual operators kHn are
given in kernel form by
kH�i�1 � �f i�t�� �Z1
2 1kh�i�1 �t1��f i�t 2 t1� dt1 for i � 1; 2
kH�i;j�2 ��f i�t�; �f j�t��
�Z1
2 1
Z1
2 1kh�i;j�2 �t1; t2� �f i�t 2 t1��f j�t 2 t2� dt1 dt2
for i � 1; 2; j � 1; 2
kH�i;j;k�3 � �f i�t�; �f j�t�; �f k�t��
�Z1
2 1
Z1
2 1
Z1
2 1kh�i;j;k�3 �t1; t2; t3�
� �f i�t 2 t1� �f j�t 2 t2� �f k�t 2 t3� dt1 dt2 dt3
for i � 1; 2; j � 1; 2; k � 1; 2 (5)
In the above kh�i�1 �t�; kh�i;j�2 �t1; t2� and kh
�i;j;k�3 �t1; t2; t3� are
the ®rst-, second- and third-order Volterra kernels, respec-
tively. For convenience, writing the Volterra operators as
kh�i�1 � kH�i�1 � �f i�t�� kh�i;j�2 � kH�i;j�2 � �f i�t�; �f j�t��
kh�i;j;k�3 � kH�i;j;k�3 ��f i�t�; �f j�t�; �f k�t��
�6�
the response of Eq. (3) can be written as
kh�t� �X
i�1;2
kh�i�1 1X
i�1;2; j�1;2
kh�i;j�2
1X
i�1;2; j�1;2; k�1;2
kh�i;j;k�3 1 ¼ �7�
3. Synthesis of higher order Volterra kernel factors
The Volterra operators are now determined as follows.
The excitation forces �f 1�t� and �f 2�t� are replaced by c �f 1�t�and c �f 2�t�; respectively, c being a constant. Noting Eq. (5),
the resulting response of the system becomes
kh�t� �X
i�1;2
ckh�i�1 1X
i�1;2; j�1;2
c2kh�i;j�2
1X
i�1;2; j�1;2; k�1;2
c3kh�i;j;k�3 1 ¼ �8�
Eq. (8) and the derivatives of its terms are substituted in
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 139
Eq. (3). Summing up the responses of equal order as
kh1 �X
i�1;2
h�i�1 ; kh2 �X
i�1;2; j�1;2
kh�i;j�2 ;
kh3 �X
i�1;2; j�1;2; k�1;2
kh�i;j;k�3 �k being x1; x2; x3��9�
and noting the following symmetry of kernels [18]
kh�i;j�2 � kh�j;i�2 ; kh�i;j;j�3 � kh�j;i;j�3 � kh�j;j;i�3 etc: �10�the governing equations can be written as
�cx1h 001 1 c2x1h 002 1 c3x1h 003��cx2h 001 1 c2x2h 002 1 c3x2h 003��cx3h 001 1 c2x3h 002 1 c3x3h 003�
8>><>>:9>>=>>; 1 2
j11 0 0
0 j22 0
0 0 j33
26643775
��cx1h 01 1 c2x1h 02 1 c3x1h 03��cx2h 01 1 c2x2h 02 1 c3x2h 03��cx3h 01 1 c2x3h 02 1 c3x3h 03�
8>><>>:9>>=>>;
1
l11 1 lLb1
l12 l13
l21 l22 1 lLb2
l23
l31 l32 l33
2666437775
��cx1h1 1 c2x1h2 1 c3x1h3��cx2h1 1 c2x2h2 1 c3x2h3��cx3h1 1 c2x3h2 1 c3x3h3�
8>><>>:9>>=>>; 1
lNb1
0 0
0 lNb2
0
0 0 0
2666437775
��cx1h1 1 c2x1h2 1 c3x1h3�3
�cx2h1 1 c2x2h2 1 c3x2h3�3
�cx3h1 1 c2x3h2 1 c3x3h3�3
8>><>>:9>>=>>;
� c
�f 1�t��f 2�t�
0
8>><>>:9>>=>>; �11�
Eq. (11) is a power series in c with coef®cients of cn beingx1hn;
x2hn or x3hn �n � 1; 2; 3�: The responses, x1hn;x2hn and
x3hn have been worked out in Appendix A, by equating the
like powers of c. The Laplace transform of the ®rst-order
response becomes
kh1�s� �X3
1
kH�i�1 �s�Fi�s� �12�
where kH�i�1 �s� is the Laplace transforms of the ®rst-order
kernel (Appendix A). The second-order response is found to
be identically equal to zero for the system under considera-
tion, i.e. kh2�s1; s2� � 0; which gives the second-order
kernel transforms as
kH�i�2 �s1; s2� � 0 �13�
The third-order response kh3; resulting due to the operation
of the third-order kernel on the excitation forces �f 1�t� and�f 2�t� can be shown (Appendix A) to be equal to a operation
of ®rst-order kernels on q1�t� and q2�t� as
kh3 � kH3� �f 1�t�; �f 2�t�� � kH1�q1; q2� �14�where
q1�t� � 2lN11
x1h31; q2�t� � 2lN
22x2h3
1 �15�Since the ®rst-order kernel operator, kH1; is linear Eq. (14)
can be written as
kH3� �f 1�t�; �f 2�t�� � 2lN11
kH�1�1 �kh31�2 lN
22kH�2�1 �kh3
1� �16�Noting that
kh1 � kH�1�1 � �f 1�t��1 kH�2�1 ��f 2�t�� �17�the Laplace transform of Eq. (16) provides an expression for
the third-order kernel transforms kH3�s1; s2; s3�; for k denot-
ing x1, x2 or x3 as
x1 H3�s1; s2; s3� � lN11�x1x1C 1±1;1;1
3 1 3x1x1C 1±1;1;23
1 3x1x1C 1±1;2;23 1 x1x1C 1±2;2;2
3 �
1 lN22�x1x2C 2±1;1;1
3 1 3x1x2C 2±1;1;23
1 3x1x2C 2±1;2;23 1 x1x2C 2±2;2;2
3 �x2 H3�s1; s2; s3� � lN
11�x2x1C 1±1;1;13 1 3x2x1C 1±1;1;2
3
1 3x2x1C 1±1;2;23 1 x2x1C 1±2;2;2
3 �
1 lN22�x2x2C 2±1;1;1
3 1 3x2x2C 2±1;1;23
1 3x2x2C 2±1;2;23 1 x2x2C 2±2;2;2
3 �x3 H3�s1; s2; s3� � lN
11�x3x1C 1±1;1;13 1 3x3x1C 1±1;1;2
3
1 3x3x1C 1±1;2;23 1 x3x1C 1±2;2;2
3 �
1 lN22�x3x2C 2±1;1;1
3 1 3x3x2C 2±1;1;23
1 3x3x2C 2±1;2;23 1 x3x2C 2±2;2;2
3 �
�18�
where x1x1C �i±j;k;l�3 �s1; s2; s3� etc. have been termed as `third-
order kernel factors' and are given in Appendix B. The
third-order kernel factors given above can be readily
constructed using equations from the ®rst-order kernelsx1 H�1�1 �s�; x1 H�2�1 �s�; x2 H�1�1 �s�; x2 H�2�1 �s�; x3 H�1�1 �s� andx3 H�2�1 �s�:
4. Measurement of Wiener kernels
Two major problems with the practical application of
Volterra Series analysis, namely, measurement of individual
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157140
Volterra kernels and convergence of Volterra series are
circumvented through usage of Wiener functionals. Wiener
kernels can be extracted from the measured response for
a Gaussian white noise excitation. These Wiener kernels
are then employed to generate the Volterra kernels. The
higher order `measured' Volterra kernels thus obtained
are equated to those obtained from the synthesis pro-
cedure described previously for nonlinear parameter
estimation.
In the present case, the Wiener kernels of the nonlinear
system are extracted by the application of white Gaussian
forces �f 1�t� and �f 2�t�; one at a time, i.e. ®rst a white Gaus-
sian force �f 1�t� with variance A1 is applied at bearing 1,
while keeping the force at bearing 2, �f 2�t� � 0: The result-
ing responses x1h; x2h and x3h are employed to extract the
direct, x1±x1 (at bearing 1), Wiener kernels and the cross
(x1±x2 and x1±x3) kernels. In the next instance, a white
Gaussian force �f 2�t� with variance A2 is applied at bearing
2 while keeping the force �f 1�t� � 0: The system responses,
in this instance, are employed to extract the direct x2-coor-
dinate Wiener kernels and the cross (x2±x1, x2±x3) kernels.
The system response in terms of Wiener operators can be
expressed in the two individual cases (with k denoting x1, x2
or x3) as
kh�t� � kW� �f 1�t�; 0� � kW��f 1�t��
when �f 1�t� is Gaussian white;
with variance A1 and �f 2�t� � 0
�19�
kh�t� � kW�0; �f 2�t�� � kW��f 2�t��
when �f 2�t� is Gaussian white;
with variance A2 and �f 1�t� � 0
�20�
In either of the two cases, (Eqs. (19) and (20)), the response
gets represented as
kh�t� � kW0 1Z1
2 1kW �i�
1 �v1� �Fi�v1�ejv1t dv1
1
"Z1 1
2 1
Z1 1
2 1kW �i�
2 �v1;v2� �Fi�v1� �Fi�v2� ej�v11v2�t dv1 dv2
2AZ1 1
2 1kW �i�
2 �v1;2v2� dv2
1Z1 1
2 1
Z1 1
2 1
Z1 1
2 1kW �i�
3 �v1;v2;v3�
£ �Fi�v1� �Fi�v2� �Fi�v3� ej�v11v21v3�t dv1 dv2 dv3
2 3AZ1 1
2 1
Z1 1
2 1kW �i�
3 �v1;v2;v2� dv1 dv2
#1 ¼
k � x1; x2; x3; i � 1; 2 (21)
where kW0;kW �i�
1 ;kW �i�
2 �v1;v2� and kW �i�3 �v1;v2;v3� are
the frequency-domain Wiener kernels of the zeroth-, ®rst-,
second- and third-order, respectively. A scheme involving a
complex exponential ®lter suggested by French and Butz
[25] as shown in Fig. 2 is employed for the extraction of
Wiener kernels from the measured response. The ®lter
output is
z�i��t� �Z1
2 1ejvt1 �f i�t 2 t1� dt1 � �Fp
i �v� e2jvt1 �22�
and the ensemble averages of the outputs of the circuit, for k
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 141
Fig. 2. Scheme for evaluation of the ®rst-order direct and cross Wiener kernel transforms, xW �i�1 :
equal to x1, x2 and x3 are
kkh�t�z�i��t�l � kW0k �Fpi �v�l e2jvt
1Z1
2 1kW �i�
1 �v1�k �Fi�v1� �Fpi �v�l e2jt�v12v� dv1
1
"Z1
2 1
Z1
2 1kW �i�
2 �v1;v2�
£ k �Fi�v1� �Fi�v2� �Fpi �v�l e2jt�v11v22v� dv1 dv2
2AikFpi �v�l e2jv1t
Z1
2 1kW �i�
2 �v2;2v2� dv2
#
1
"Z1
2 1
Z1
2 1
Z1
2 1kW �i�
3 �v1;v2;v3�
£ k �Fi�v1� �Fi�v2� �Fi�v3� �Fpi �v�l e2jt�v11v21v32v� dv1 dv2 dv3
23Ai
Z1
2 1
Z1
2 1kW �i�
3 �v1;v2;2v2�
£ k �Fpi �v1� �Fp
i �v�l e2jt�v12v� dv1 dv2
#1 ¼ (23)
Employing the properties [33] of the ensemble averages of
products of the stationary Gaussian white noise process�Fi�v�; Eq. (23) gets reduced, after some algebra, to
kkh�t�z�i��t�l � AikW �i�
1 �v� �24�However, due to the equivalence of time and ensemble
averages, the ensemble average kkh�t�z�i��t�l can also be
written as
kkh�t�z�i��t�l � limT!1
1
T
ZT=2
2 T =2
kh�t�z�i��t� dt � �Fpi �v�kh�v�
�25�Eqs. (24) and (25) give
AikW �i�
1 �v� � �Fpi �v�kh�v� �26�
from which the expression for the ®rst-order Wiener kernel
transform is obtained as
kW �i�1 �v� � �Fi�v�kh�v�=Ai �27�
Since k takes values x1, x2, x3 and i takes values 1 and 2
the direct kernels x1 W �1�1 �v�; x2 W �2�
1 �v� and the cross kernelsx1 W �2�
1 �v�; x2 W �1�1 �v�; x3 W �1�
1 �v� and x3 W �2�1 �v� can be
extracted from the measured responses x1h�v�; x2h�v�;x3h�v� and the applied force � �F1�v� and its variance A1 or�F2�v� and its variance A2), through Eq. (27).
For measurement of the third-order kernel, a circuit invol-
ving three exponential delay ®lters as shown in Fig. 3 is
considered. The output, z�i��t�; of the exponential ®lters is
z�i��t� �Z1
2 1e2jv1t1 �f i�t 2 t1� dt1
�Z1
2 1e2jv2t2 �f i�t 2 t2� dt2
�Z1
2 1e2jv3t3 �f i�t 2 t3� dt3
� �Fi�2v1� �Fi�2v2� �Fi�2v3� e2j�v11v21v3�t (29)
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157142
Fig. 3. Scheme for evaluation of the third-order direct and cross Wiener kernel transforms, xW �i�3 �v;v;v�:
and the ensemble averages of the outputs of the circuit are
kkh�t�z�i��t�l � �A2i �kW �i�
1 �v1�d�2v2 2 v3� ej�2v22v3�t
1 kW �i�1 �v2�d�2v1 2 v3� ej�2v12v3�t
1 kW �i�1 �v3�d�2v1 2 v2� ej�2v12v2�t�
1 �6A3ikW �i�
3 �v1;v2;v3�� �29�
However, the equivalence of time and ensemble averages
gives
kkh�t�z�i��t�l � limT!1
1
T
ZT=2
2 T=2
kh�t�z�i��t� dti
� �Fi�2v1� �Fi�2v2� �Fi�2v3�kh�v1 1 v2 1 v3� �30�
Eqs. (29) and (30) give the expression for the measurement
of the third-order Wiener kernel transform as
kW �i�3 �v1;v2;v3�
� 1
6A3i
� �Fpi �v1� �Fp
i �v2� �Fpi �v3�x1h�v1 1 v2 1 v3��
21
6Ai
�kW �i�1 �v1�d�v2 1 v3�1 kW �i�
1 �v2�d�v1 1 v3�
1 kW �i�1 �v3�d�v1 1 v2�� (31)
The third-order kernels, x1 W �i�3 �v1;v2;v3�; x2 W �i�
3 �v1;v2;v3�and x3 W �i�
3 �v1;v2;v3� form multi-dimensional surfaces on
the �v1;v2;v3� axes. Measurements are made for special
tri-spectral kernels with v1 � v2 � v3 � v: These kernels
being functions of only one variable v , are easier to
compute and interpret. For such tri-spectral kernels the
expression (31) reduces to
kW �i�3 �v;v;v� �
1
6A3i
�{ �Fpi �v�}3kh�3v��
21
2Ai
�kW �i�1 �v��d�v� �32�
5. Parameter estimation
The ®rst-order Wiener kernels kW �i�1 �v� and the third-
order Special Tri-spectral Wiener kernels kW �i�3 �v;v;v�
are estimated using Eqs. (27) and (32), respectively, from
the measurements of spectral component F�v� of the excita-
tion force, its variance Ai and the spectral componentskh�v�; kh�3v� of the corresponding response. Subsequently,
for a third-order representation of the system response,
noting the orhogonality property [18] between Volterra
and Wiener kernels, the ®rst and Special Tri-spectral
Volterra kernel transforms can be computed as
kH�i�3 �v;v;v� � kW �i�3 �v;v;v�
kH�i�1 �v� � kW �i�1 �v�1 kW �i�
1�3��v��33�
where
kW �i�1�3��v� �
Z1
2 1kW �i�
3 �v;v2;2v2� dv2
The linear parameters can be obtained from the above esti-
mates of the ®rst-order Volterra kernels kH�i�1 �v�: Noting
the algebraic expressions of these kernels from Appendix
A, the linear stiffness parameters of the bearings lb1and lb2
are estimated through a complex curve ®tting routine [35].
In addition, the shaft stiffnesses and damping ratios lij; j ij
i � 1; 2; 3; j � 1; 2; 3 are also obtained from the curve
®t routine.
The nonlinear parameters are computed from the
estimates of the Special Tri-spectral Volterra kernelsx1 H�1�3 �v;v;v�; x1 H�2�3 �v;v;v�; x2 H�1�3 �v;v;v�; x2 H�2�3
�v;v;v�; x3 H�1�3 �v;v;v� and x3 H�2�3 �v;v;v�: Since these
kernels are estimated by application of a single white Gaus-
sian force at a time, the synthesised expressions (18), for the
third-order Volterra kernels also get reduced in the two
individual cases to�f 1�t� Gaussian white, with variance A1 and �f 2�t� � 0 :
x1 H3�v;v;v� � lN11�x1x1C 1±1;1;1
3 �1 lN22�x1x2C 2±1;1;1
3 �x2 H3�v;v;v� � lN
11�x2x1C 1±1;1;13 �1 lN
22�x2x2C 2±1;1;13 �
x3 H3�v;v;v� � lN11�x3x1C 1±1;1;1
3 �1 lN22�x3x2C 2±1;1;1
3 �
�34�
�f 2�t� Gaussian white, with variance A2 and �f 1�t� � 0 :
x1 H3�v;v;v� � lN11�x1x1C 1±2;2;2
3 �1 lN22�x1x2C 2±2;2;2
3 �x2 H3�v;v;v� � lN
11�x2x1C 1±2;2;23 �1 lN
22�x2x2C 2±2;2;23 �
x3 H3�v;v;v� � lN11�x3x1C 1±2;2;2
3 �1 lN22�x3x2C 2±2;2;2
3 �
�35�
While application of two forces (individually) is required
for estimation of the linear cross coupling terms, only two
equations out of the set of six in expressions (34) and (35)
are suf®cient for the estimation of the two nonlinear
unknowns l 11N and l 22
N (cross-coupled nonlinear parameters
l 12N , l 13
N and l 23N being taken zero). Estimation of l 11
N and l 22N
has been carried out here, using the ®rst two equations from
the set (34). For these two equations, we have
1
6A31
�{ �Fp1�v�}3x1h�3v��2
1
2A1
�x1 W �1�1 �v�d�v��
� lN11�x1x1C 1±1;1;1
3 �1 lN22�x1x2C 2±1;1;1
3 �1
6A31
�{ �Fp1�v�}3x2h�3v��2
1
2A1
�x2 W �1�1 �v�d�v��
� lN11�x2x1C 1±1;1;1
3 �1 lN22�x2x2C 2±1;1;1
3 �
�36�
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 143
The above are solved simultaneously for l 11N and l 22
N (the
third-order kernel factors, C , are known from the estimates
of the ®rst-order kernels and relationships given in
Appendix B).
6. Computer simulation
The procedure is illustrated through numerical simu-
lation of the response of the non-dimensional Eq. (3).
The shaft stiffness matrix for the simply supported system,
carrying a centrally located disc as (refer Fig. 1 for
station numbering) is computed using strength of materials
formulae [34]
k11 k12 k13
k21 k22 k23
k31 k32 k33
26643775 � 12EI
l3
1 0 21
0 1 21
21 21 2
26643775 �37�
which gives the non-dimensionalised matrix
l11 1 lb1l12 l13
l21 l22 1 lb2l23
l31 l32 l33
26643775
��0:5 1 lb1
�=m1 0 2�0:5=m1�0 �0:5 1 lb2
�=m2 2�0:5=m2�20:5 20:5 1
26643775 �38�
where m 1 and m 2 are equal to the mass ratios m1=m3 and
m2=m3; respectively. In the rotor con®guration shown in Fig.
1, m1 and m2 are the masses effectively seen by the sensors at
the bearing ends and will be small in magnitude in compar-
ison to m3. However, for simplicity in numerical simulation
the mass ratios m1=m3 and m2=m3 are chosen to be each equal
to 1.0. The values of the individual elements of the above
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157144
Fig. 4. (a) Typical sample of input force. (b) Power-spectrum of the input force (averaged over 2000 samples).
lambda matrix therefore become
l11 � l22 � 0:5 l33 � 1:0 l12 � l21 � 0
l13 � l23 � 20:5 l31 � l32 � 20:5
In order to illustrate the numerical results when shaft and
bearing stiffness are both equally signi®cant numerically,
the values of the linear bearing stiffness parameters are
taken as
lb1� 0:5 lb2
� 1:0
The nonlinear parameters are chosen as
lNb1� 0:1 lN
b2� 0:1
Damping is chosen as j11 � j22 � j33 � 0:01 in all the
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 145
Fig. 5. Typical response samples. (a) Response x1h�t� at station 1. (b) Response x2h�t� at station 2. (c) Response x3h�t� at station 3.
cases. The excitation forces are simulated through random
number generating subroutines and are normalised with
respect to the maximum value of f1�t�: A typical sample
of the excitation is shown in Fig. 4a. The power spectrum
of the input averaged over an ensemble of 2000 force
samples is shown in Fig. 4b. Responses x1h; x2h and x3h
are generated numerically for 4096 number of instances in
the non-dimensional time (t) range 0±2048, by solving the
governing equations through fourth-order Runge±Kutta
subroutine. The responses are computed for 2000 number
of samples of the simulated random force and fed as inputs
to the parameter estimation algorithm. The various ®rst- and
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157146
Fig. 6. Power-spectra of the response (averaged over 2000 samples) of: (a) x1h�t�; (b) x2h�t�; and (c) x3h�t�:
higher order kernels are extracted from the responses and
consequently parameter estimation is carried out. The
output consists of the linear stiffness parameters lb1; lb2
;
the damping ratios j 11, j 22, j 33, the mass ratios m 1, m 2 and
the nonlinear stiffness parameters lNb1
and lNb2: The esti-
mated parameters are compared with those originally used
for the simulation of response and the accuracy of estimates
and errors involved are discussed.x1h; x2h and x3h numerically resulting from the force of
Fig. 4a and b, applied at station are shown in Fig. 5a±c (no
force is applied at the second bearing.) The corresponding
power-spectra are shown in Fig. 6a±c. The fundamental
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 147
Fig. 7. Estimates of the ®rst-order kernel transforms of: (a) x1 H�1�1 �v�; (b) x2 H�1�1 �v�; (c) x3 H�1�1 �v�; (d) x1 H�2�1 �v�; (e) x2 H�2�1 �v�; and (f) x3 H�2�1 �v�:
frequencies of the system can be noticed from these ®gures
to exist at 0.097, 0.175 and 0.219 cycles/t . The frequencies
correspond to those obtained from the eigenvalue solution
of the linear non-dimensional stiffness matrix described in
Eqs. (37) and (38) and can be called v 1, v 2, v 3. It can also
be noticed from the power-spectra of Fig. 6a±c that the
system nonlinearity is not apparently, equally displayed
by responses x1h; x2h and x3h: The plot of x2h (Fig. 6b)
displays additional peaks at frequencies 0.263, 0.291,
0.369, 0.490, 0.525 and 0.560 cycles/t , which can be iden-
ti®ed as �2v3 2 v2�; (3v 1), �2v1 1 v2�; �v1 1 v2 1 v3�;(3v 2) and �2v2 1 v3� harmonics, respectively. These
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157148
Fig. 7. (continued)
harmonics are not distinctly visible in the plots of x1h (Fig.
6a) and x3h (Fig. 6c). This is due to the fact that stations 1
and 3, being closer to the station of force application (station
1), the linear response levels are higher at these stations in
comparison to that at station 2 and overlap the nonlinear
contributions. Similar response plots can be obtained by
application of the force at station 2, while keeping the
force at station 1 equal to zero.
The applied force and resultant response at the three
stations are employed in Eqs. (27) and (32) to extract the
®rst-order Volterra kernels, kH�i�1 �v� shown in Fig. 7a±f.
These kernels show the three fundamental frequencies of
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 149
Fig. 8. Normalised error in the ®rst-order estimates of: (a) x1 H�1�1 �v�; (b) x2 H�1�1 �v�; (c) x3 H�1�1 �v�; (d) x1 H�2�1 �v�; (e) x2 H�2�1 �v�; and (f) x3 H�2�1 �v�:
the system, mentioned above. The errors in these estimated
kernels, is given in Fig. 8a±f. The errors are computed by
comparing the estimated kernels with those obtained from
the exact analytical expressions (Appendix A). The errors,
as expected [36], are high in the vicinity of the fundamental
frequencies. However, they are in the 10% zone up to a non-
dimensional frequency of 0.06 cycles/t . Parameter estima-
tion is carried out in this frequency range.
The third-order kernel factors x1x1C 1±1;1;13 �v;v;v�;
x1x2C 2±1;1;13 �v;v;v�; x2x1C 1±1;1;1
3 �v;v;v�; x2x2C 2±1;1;13
�v;v;v�, x3x1C 1±1;1;13 �v;v;v� and x3x2C 2±1;1;1
3 �v;v;v�synthesised from the ®rst-order kernels are shown in Fig.
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157150
Fig. 8. (continued)
9a±f. The third-order kernels x1 H�1�3 �v;v;v�; x2 H�1�3 �v;v;v�and x3 H�1�3 �v;v;v�; extracted from the measurements of the
force and response, in accordance with Eqs. (32) and (33)
are shown in Fig. 10a±c. While the ®rst-order kernels are
estimated in the entire available frequency range 0.0±1.0,
the third-order kernels involving a 3v factor, have to be
restricted to one-third of this frequency zone (i.e. 0.0±
0.33). It can be observed from the ®gures that while the
measured third-order kernels are reasonably accurate in
showing the harmonic at v1;2;3=3 (at non-dimensional
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 151
Fig. 9. Estimates of the third-order kernel factors of: (a) x1x1C 121;1;13 �v;v;v�; (b) x1x2C 221;1;1
3 �v;v;v�; (c) x2x1C 121;1;13 �v;v;v�; (d) x2x2C 221;1;1
3 �v;v;v�; (e)x3x1C 121;1;1
3 �v;v;v�; and (f) x3x2C 221;1;13 �v;v;v�:
frequencies� 0.032, 0.058 and 0.073 cycles/t ), identi®ca-
tion of the harmonics at v 1,2,3 (at non-dimensional
frequencies� 0.097, 0.175, 0.219 cycles/t) is weak, due
to higher statistical errors. The estimation of nonlinear para-
meters l 11N and l 22
N from these kernels is therefore restricted
to the frequency zone of 0.0±0.07.
The estimates of the nonlinear parameter l 11N and l 22
N ,
obtained in accordance with the relationship (36), are
shown in Fig. 11a and b. A fourth-order polynomial
curve regressed through the estimates of these nonlinear
parameters over the frequency range is also shown in
these ®gures. The mean values of the estimates are
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157152
Fig. 9. (continued)
found to be
lNb1� 0:09 lN
b2� 0:12
(The exact values of the above nonlinear parameters
are those chosen for response simulation, that is,
lNb1� lN
b2� 0:10�: The linear parameters have been
estimated from the ®rst-order kernels of Fig. 7a±f,
using a complex curve ®tting routine [35]. The estimates
are
m1 � 0:956 m2 � 0:897
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 153
Fig. 10. Estimates of third-order kernel transforms of: (a) x1 H�1�3 �v;v;v�; (b) x2 H�1�3 �v;v;v�; and (c) x3 H13 �v;v;v�:
lb1� 0:487 lb2
� 0:898
j11 � j22 � j33 � 0:011
7. Remarks
Reasonably good estimates have been obtained through
numerical illustration of the proposed procedure. The accu-
racy lies within the 10% zone for all the parameters. It is to
be noted that the response representation has been restricted
to third-order kernels only, in this study. Also, the ensemble
size has been restricted to 2000.
Acknowledgements
The authors wish to express their thanks to the ®nancial
aid being provided by the Propulsion Panel of Aeronautical
Research and Development Board, Ministry of Defence,
Government of India, in carrying out the study.
Appendix A. Synthesis of kernel transforms
Equating the like powers of c in Eq. (11)
c1 terms:
x1h 001x2h 001x3h 001
8>><>>:9>>=>>;1 2
j11 0 0
0 j22 0
0 0 j33
26643775
x1h 01x2h 01x3h 01
8>><>>:9>>=>>;
1
l11 1 lLb1
l12 l13
l21 l22 1 lLb2
l23
l31 l32 l33
2666437775
x1h1
x2h1
x3h1
8>><>>:9>>=>>; �
�f 1�t��f 2�t�
0
8>><>>:9>>=>>;�A1�
c2 terms:
x1h 002x2h 002x3h 002
8>><>>:9>>=>>;1 2
j11 0 0
0 j22 0
0 0 j33
26643775
x1h 02x2h 02x3h 02
8>><>>:9>>=>>;
1
l11 1 lLb1
l12 l13
l21 l22 1 lLb2
l23
l31 l32 l33
2666437775
x1h2
x2h2
x3h2
8>><>>:9>>=>>; �
0
0
0
8>><>>:9>>=>>; �A2�
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157154
Fig. 11. Estimates of the nonlinear parameters of: (a) lNb1; and (b) lN
b2:
c3 terms:
x1h 003x2h 003x3h 003
8>><>>:9>>=>>; 1 2
j11 0 0
0 j22 0
0 0 j33
26643775
x1h 03x2h 03x3h 03
8>><>>:9>>=>>;
1
l11 1 lLb1
l12 l13
l21 l22 1 lLb2
l23
l31 l32 l33
2666437775
x1h3
x2h3
x3h3
8>><>>:9>>=>>;
1
lNb1
0 0
0 lNb2
0
0 0 0
2666437775
x1h31
x2h31
x3h31
8>><>>:9>>=>>; �
0
0
0
8>><>>:9>>=>>; �A3�
Eqs. (A1)±(A3) can be solved sequentially. Taking Laplace
transforms of Eq. (A1), for zero initial conditions, one
obtains
�M�{h1�s�} � {F�s�}
with
�M� �
s2 1 2sj11 1 l11 1 lLb1
l12 l13
l21 s2 1 2sj22 1 l22 1 lLb2
l23
l31 l32 s2 1 2sj33 1 l33
2666437775
�A4�
{h1�s�} � { x1h1�s� x2h1�s� x3h1�s�}T
and {F�s�} � { F1�s� F2�s� 0}T
The solution for x1h1�s�; x2h1�s� and x3h1�s� from the above
is
{h1�s�} � �H�{F�s�} �A5�
where the kernel matrix
�H� � �M�21 �A6�
whose individual elements can be worked out to be
�H� �x1 H1�s� x1 H2�s� x1 H3�s�x2 H1�s� x2 H2�s� x2 H3�s�x3 H1�s� x3 H2�s� x3 H3�s�
2666437775
x1 H1�s� � �2l23l32 1 �s2 1 2sj22 1 l22 1 lLb2�
� �s2 1 2sj33 1 l33��=Dx1 H2�s� � �l13l32 2 l12�s2 1 2sj33 1 l33��=Dx1 H3�s� � �2l13�s2 1 2sj22 1 l22 1 lL
b2�1 l12l33�=D
x2 H1�s� � �l23l31 2 l21�s2 1 2sj33 1 l33��=Dx2 H2�s� � �2l13l31 1 �s2 1 2sj11 1 l11 1 lL
b1�
� �s2 1 2sj33 1 l33��=Dx2 H3�s� � �l13l21 2 �s2 1 2sj11 1 l11 1 lL
b1�l23�=D
x3 H1�s� � �2�s2 1 2sj22 1 l22 1 lLb2�l31 1 l21l32�=D
x3 H2�s� � �l12l31 2 �s2 1 2sj11 1 l11 1 lLb1�l32�=D
x3 H3�s� � �2l12l21 1 �s2 1 2sj11 1 l11 1 lLb1�
� �s2 1 2sj22 1 l22 1 lLb2��=D (A7)
with
D � �s2 1 2sj11 1 l11 1 lLb1�
� �s2 1 2sj22 1 l22 1 lLb2��s2 1 2sj33 1 l33�
2 �s2 1 2sj11 1 l11 1 lLb1�l23l32
2 l13�s2 1 2sj22 1 l22 1 lLb2�l31
2 l12l21�s2 1 2sj33 1 l33�1 l12l23l31 1 l13l21l32
�A8�Taking the Laplace transform of Eq. (A2) similarly gives
s2 1 2sj11 1 l11 1 lLb1
l12 l13
l21 s2 1 2sj22 1 l22 1 lLb2
l23
l31 l32 s2 1 2sj33 1 l33
2666437775
�x1h2�s�x2h2�s�x3h2�s�
8>><>>:9>>=>>; �
0
0
0
8>><>>:9>>=>>; (A9)
which yields
x1h2�s� � 0; x2h2�s� � 0; x3h2�s� � 0 �A10�which shows that the second-order kernel is identically zero,
i.e.
x1 k2�t1; t2� � x2 k2�t1; t2� � x3 k2�t1; t2� � 0 �A11�In order to synthesise expressions for third-order kernels,
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 155
Eq. (A3) can be written as
x1h 003x2h 003x3h 003
8>><>>:9>>=>>;1 2
j11 0 0
0 j22 0
0 0 j33
26643775
x1h 03x2h 03x3h 03
8>><>>:9>>=>>;
1
l11 1 lLb1
l12 l13
l21 l22 1 lLb2
l23
l31 l32 l33
2666437775
x1h3
x2h3
x3h3
8>><>>:9>>=>>;
�q1�t�q2�t�
0
8>><>>:9>>=>>; �A12�
where the following abbreviations have been used:
q1�t� � 2lN11
x1h31�t�; q2�t� � 2lN
22x2h3
1�t� �A13�Eq. (A12) is a set of linear equations, similar to Eq. (A3)
and therefore the solution in terms of Volterra operators can
be written as
x1h3�t� � x1 H1�q1; q2�;x2h3�t� � x2 H1�q1; q2�;x3h3�t� � x3 H1�q1; q2�
�A14�
that is
x1 H3� �f 1�t�; �f 2�t�� � x1 H1�q1; q2�x2 H3� �f 1�t�; �f 2�t�� � x2 H1�q1; q2�x3 H3� �f 1�t�; �f 2�t�� � x3 H1�q1; q2�:
�A15�
Appendix B. Third-order kernel factors
x1x1C �i±j;k;l�3 �s1; s2; s3�
� 2x1 H�i�1 �s1 1 s2 1 s3�x1 H�j�1 �s1�x1 H�k�1 �s2�x1 H�l�1 �s3�
x2x2C �i±j;k;l�3 �s1; s2; s3�
� 2x2 H�i�1 �s1 1 s2 1 s3�x2 H�j�1 �s1�x2 H�k�1 �s2�x2 H�l�1 �s3�
x2x1C �l±i;j;k�3 �s1; s2; s3�
� 2x2 H�l�1 �s1 1 s2 1 s3�x1 H�i�1 �s1�x1 H�j�1 �s2�x1 H�k�1 �s3�
x3x1C �i±j;k;l�3 �s1; s2; s3�
� 2x3 H�i�1 �s1 1 s2 1 s3�x1 H�j�1 �s1�x1 H�k�1 �s2�x1 H�l�1 �s3�
x3x2C �l±i;j;k�3 �s1; s2; s3�
� 2x3 H�l�1 �s1 1 s2 1 s3�x2 H�i�1 �s1�x2 H�j�1 �s2�x2 H�k�1 �s3�
i � 1; 2; j � 1; 2; k � 1; 2; l � 1; 2:
References
[1] Nayfeh AH. Parametric identi®cation of nonlinear dynamic systems.
Computers & Structures 1985;20:487±93.
[2] Choi D, Miksad RW, Powers EW. Application of digital cross-bispec-
tral analysis techniques to model the nonlinear response of a moored
vessel system in random seas. Journal of Sound and Vibration
1985;99(3):309±26.
[3] Bendat JS, Piersol AG. Random data analysis and measurement
procedures. New York: Wiley-Interscience, 1986.
[4] Bendat JS, Palo PA, Coppolino RN. A general identi®cation techni-
que for nonlinear differential equations of motion. Probabilistic Engi-
neering Mechanics 1992;7:43±61.
[5] Bendat JS, Piersol AG. Spectral analysis of nonlinear systems invol-
ving square-law operations. Journal of Sound and Vibration
1982;81(2):199±213.
[6] Bendat JS, Piersol AG. Decomposition of wave forces into linear and
nonlinear components. Journal of Sound and Vibration
1986;106(3):391±408.
[7] Rice HJ, Fitzpatrick JA. A generalised technique for spectral analysis
of nonlinear systems. Mechanical Systems and Signal Processing
1988;2(2):195±207.
[8] Rice HJ, Fitzpatrick JA. A procedure for the identi®cation of linear
and nonlinear multi-degree-of-freedom systems. Journal of Sound and
Vibration 1991;149(3):397±411.
[9] Mohammad KS, Worden K, Tomlinson GR. Direct parameter estima-
tion for linear and nonlinear structures. Journal of Sound and Vibra-
tion 1992;152(3):471±99.
[10] Masri SF, Caughy TK. A nonparametric identi®cation technique for
nonlinear dynamic problems. Transactions of ASME, Journal of
Applied Mechanics 1979;46:433±47.
[11] Masri SF, Sassi H, Caughy TK. Nonparametric Identi®cation of
nearly arbitrary nonlinear systems. Transactions of ASME, Journal
of Applied Mechanics 1982;49:619±27.
[12] Udwadia FE, Kuo CP. Nonparametric identi®cation of a class of
nonlinear close-coupled dynamic systems. Earthquake Engineering
and Structural Dynamics 1981;9:385±409.
[13] Masri SF, Miller RK, Saud AF, Caughy TK. Identi®cation of
nonlinear vibrating structures. Part IÐformulation. Transactions of
ASME, Journal of Applied Mechanics 1987;54:918±22.
[14] Masri SF, Miller RK, Saud AF, Caughy TK. Identi®cation of
nonlinear vibrating structures. Part IIÐapplications. Transactions
of ASME, Journal of Applied Mechanics 1987;54:923±9.
[15] Volterra V. Theory of functionals. Glasgow: Blackie and Sons, 1930.
[16] Volterra V. Theory of functionals and of integral and integro-differ-
ential equations. New York: Dover, 1959.
[17] Wiener N. Nonlinear problems in random theory. New York: Wiley,
1958.
[18] Schetzen M. The Volterra and Wiener theories of nonlinear systems.
New York: Wiley, 1980.
[19] Barret JF. The use of functionals in the analysis of nonlinear physical
systems. Journal of Electronic Control 1963;15:567±615.
[20] Barret JF. The use of Volterra series to ®nd region of stability of a
nonlinear differential equation. International Journal of Control
1965;1:209.
[21] Flake RH. Volterra series representation of nonlinear systems. IEEE
Transactions on Applications in Industry 1963;81:810±5.
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157156
[22] Schetzen M. Measurement of the kernels of a nonlinear system of
®nite order. International Journal of Control 1965;1(3):251±63.
[23] Sandberg A, Stark L. Wiener G-function analysis as an approach to
nonlinear characteristics of human pupil light re¯ex. Brain Research
1968;11:194±211.
[24] Bedrosian E, Rice SO. The output properties of Volterra systems
(nonlinear system with memory) driven by harmonic and Gaussian
inputs. Proceedings of the IEEE 1971;59(12):1688±707.
[25] French AS, Butz EG. Measuring the Wiener kernels of a nonlinear
system using the fast Fourier transform algorithm. International Jour-
nal of Control 1973;17(3):529±39.
[26] French AS, Butz EG. The use of Walsh functions in the Wiener
analysis of nonlinear systems. IEEE Transactions on Computers
1974;C-23(3):225±32.
[27] Gifford SJ, Tomlinson GR. Recent advances in the application of
functional series to nonlinear structures. Journal of Sound and Vibra-
tion 1989;135(2):289±317.
[28] Haber R. Structural identi®cation of quadratic block-oriented models
based on estimated Volterra kernels. International Journal of Systems
Science 1989;20(8):1355±80.
[29] Nam SW, Kim SB, Powers EJ. Nonlinear system identi®cation with
random excitation using third order volterra series, Proceedings of 8th
International Modal Analysis Conference, 1990. p. 1278±83.
[30] Koukoulas P, Kalouptsidis N. Nonlinear system identi®cation using
Gaussian inputs. IEEE Transactions on Signal Processing
1995;43(8):1831±41.
[31] Tomlinson GR, Manson G, Lee GM. A simple criterion for establish-
ing an upper limit to the harmonic excitation level of the Duf®ng
oscillator using the Volterra series. Journal of Sound and Vibration
1996;190(5):751±62.
[32] Khan AA, Vyas NS. Nonlinear parameter estimation using Volterra and
Wiener theories. Journal of Sound and Vibration 1999;221(5):805±21.
[33] Raemer HR. Statistical communication theory and applications.
Englewood Cliffs, NJ: Prentice-Hall, 1969.
[34] Childs D. Turbomachinery rotordynamics: phenomena, modeling and
analysis. New York: Wiley, 1993.
[35] Levy EC. Complex curve ®tting, IRE Transactions on Automatic
Control 1959;AC-4:37±44.
[36] Bendat JS. Nonlinear system analysis and identi®cation from random
data. New York: Wiley, 1990.
A.A. Khan, N.S. Vyas / Probabilistic Engineering Mechanics 16 (2001) 137±157 157