Hysteretic Damping Modelling by Nonlinear Kelvin-Voigt Model
Hysteretic Damping Modelling by Nonlinear Kelvin-Voigt Model
Hysteretic Damping Modelling by Nonlinear Kelvin-Voigt Model
PUBLISHING HOUSE
OF THE ROMANIAN ACADEMY
1. INTRODUCTION
The strong dependence of the soils dynamic
properties on strain or stress level produced by external loads is very well known. In the previous
author's papers [1], [2], [3] this nonlinear behaviour was modeled assuming that the geological
materials are nonlinear viscoelastic materials. The
dynamic model obtained was built upon two dynamic nonlinear functions one for material
strength modeling and another including material
damping, both in terms of strain level caused by
external loading conditions and both functions being completely determined from resonant column
test data.
The resonant column system can be considered
as a one degree-of-freedom system that is made up
of a single mass (the vibration device) supported
by a spring and a damper represented by the
specimen [3]. But, due to the mechanical properties of the specimen materials both spring and
damper have non-linear characteristics and thus the
entire system is a non-linear one [4].
In linear dynamics a usual description of a solid
single-degree-of-freedom behaviour is given by the
Kelvin-Voigt model consisting of a spring (with a
stiffness k) and a dashpot (with a viscosity c) connected in parallel. The governing equation of this
system for torsional harmonic vibrations (usually
resonant column system excitation) is:
J 0 && + c & + k = M 0 sin t
__________________________
Recommended by Radu P.VOINEA
Member of the Romanian Academy
(1.1)
(1.2)
Mt = M0 sin t
m ; J0
k = k ()
c = c()
Using the same method that describes the nonlinearity by strain dependence of the material parameters, we assume that the damper viscosity c
and the spring stiffness k are functions in terms of
rotation [4], [5] (fig.2.2):
c ( ) = 2 J 0 0 D ( ) [Nms]
k ( ) =
Ip
h
G ( )
(2.3)
[Nm]
where 0 is the system undamped natural pulsation, Ip = 4 /32 is the polar moment of the specimen and (, h) are the diameter and height of the
cylindrical specimen. For the linear systems, the
undamped natural pulsation 0 is defined in terms
of spring stiffness k : 0 = k / J 0 . In this
case, the spring stiffness is a function, and we de-
k (0) : 0 =
k (0) / J 0 .
(3.1)
+ C ( ) + K ( ) = sin
(3.2)
where the superscript accent denotes the time derivative with respect to , and:
C () = C() =
K () = K () =
=
M0
J0
2
0
c()
= 2 D ()
J 00
k ()
k () G ()
=
=
= G n ( ) (3.3)
2
J 0 0
k (0 ) G (0 )
=
M0
k (0 )
= st
(3.4)
A
ra 2
(3.5)
1 W
4 W
(4.1)
Using the same single degree-of-freedom system from fig.1.1 there is a possibility to compare
the resonant column experimental damping values
with the values obtained from non-linear KelvinVoigt model and Masing model.
We mention that in the ordinary resonant column test the damping evaluation uses a different
method the magnification factor method based
on measuring both current and acceleration at two
different frequencies - from resonant frequency f r
and at 2 f r .
To verify the capabilities of the non-linear Kelvin-Voigt equation (1.2) to modelling a hysteresis
loop one can use a inverse strategy starting from
the given dynamic material functions c = c ( )
and k = k ( ) included in the restoring force
Q = Q , & one can built the hysteresis loops for a
( )
( )
( )
(4.2)
(4.3)
& = 0 sin t
(4.4)
and, then:
(4.5)
(4.6)
4. CONCLUDING REMARKS
2.
3.
4.
5.
6.
7.
8.
9.
ACKNOWLEDGEMENTS
10.
11.
12.
REFERENCES
1.
13.