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Faculty of Engineering
2015
Page 1
Tuned liquid dampers Abd Elrahman Abd Elbasst Elborolossy, Department of Civil Engineering,
Faculty of Engineering, Tanta University, Egypt
E-mail: [email protected]
Abstract - Current trends in construction industry demands taller and lighter structures, which are also more flexible and having quite low damping value. This increases failure possibilities and also, problems from serviceability point of view. Several techniques are available today to minimize the vibration of the structure, out of which concept of using of TLD is a newer one. This study was made to study the effectiveness of using TLD for controlling vibration of structure.
- A TLD (tuned liquid damper) is a passive control devise on top of a structure that dissipates the input excitation energy through the liquid boundary layer friction, the free surface contamination, and wave breaking. In order to design an efficient TLD, using an appropriate model to illustrate the liquid behavior as well as knowing optimum TLD parameters is of crucial importance. - In this study the accuracy of the existing models which are able to capture the liquid motion behavior are investigated and the effective range of important TLD parameters are introduced through real-time hybrid shaking table tests.
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2015
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History: Since 1950s liquid dampers have been used to stabilize marine vessels or to control wobbling motion of satellites. In the late 1970s TLD has started to be used in civil engineering to reduce structural motion; Vandiver and Mitome (1979) used TLD to reduce the wind vibration of a platform. Also, Mei (1978) and Yamamoto et al. (1982) looked into structure-wave interactions using numerical methods. In the early 1980s important parameters such as liquid height, mass, frequency, and damping for a TLD attached to offshore platforms were studied by Lee and Reddy (1982). Bauer (1984) introduced a rectangular tank full of two immiscible liquids to a building structure. Kareem and Sun (1987), Sato (1987), Toshiyuki and Tanaka, and Modi and Welt (1987) were among the first researchers who suggested using TLD in civil structures.Wakahara et al. (1992) and Tamamura et al. (1995) showed the effectiveness of TLDs installed in real structures such as Nagasaki airport tower, Yokohama Marine tower, and Shin Yokohama Prince (SYP) hotel to reduce the structural vibration.
Lateral load resistance :-
1- Structural modifications. 2- Aerodynamic modifications. 3- Base isolation techniques.
4- Damping sources.
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2015
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Damping sources :- 1- Structural.
2- Aerodynamic.
3- Soil.
4- Auxiliary " supplemental
Supplemental Damping Systems:-
Supplemental damping system can be categorized in three groups as passive, active and semi-active systems. These dampers are activated by the movement of structure and decrease the structural displacements by dissipating energy via different mechanisms
Active Systems. Active systems monitor the structural behavior, and after processing the information, in a short time, generate a
set of forces to modify the current state of the structure.
Generally, an active control system is made of three
components: a monitoring system that is able to perceive the
state of the structure and record the data using an electronic
data acquisition system; a control system that decides the
reaction forces to be applied to the structure based on the from
monitoring system and; an actuating system that applies the
physical forces to the structure. To accomplish all these, an
active control system needs continuous external power source.
The loss of power that might be experienced during a
catastrophic event may render these systems output data
ineffective.
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2015
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Semi-Active Systems.
Semi-active systems are similar to active systems except that compared to active ones they need less amount of external power. Instead of exerting additional forces to the structural systems, semi-active systems control the vibrations by modifying structural properties (for example damping modification by controlling the geometry of orifices in a fluid damper). The need for external power
Passive Mechanism. Seismic input energy without any need for external power source. Their properties are constant during the seismic motion of the structure and cannot be modified. Passive control devices have been shown to work efficiently; they are robust and cost-effective. As such, they are widely used in civil engineering structures. The main categories of the passive energy dissipation systems can be seen in Table (Christopoulos and Filiatrault 2006)
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2015
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Displacement-activated devices absorb energy through the relative displacement between the points they connect to the structure. Their behaviour is usually independent of the frequency of the motion and is in phase with the maximum internal forces generated at the end of each vibration cycle corresponding to the peak deformations of the structure. Metallic dampers, friction dampers, self-centering dampers, and viscoelastic dampers are the main devices in this group.
Velocity-activated
devices absorb energy through the relative velocity between their connection points. The behaviour of these dampers is usually dependent on the frequency of the motion and out-of-phase with the maximum internal forces generated at the end of each vibration cycle corresponding to the peak deformations of the structure. This causes a lower level of design forces for structural members and foundation. Viscous and viscoelastic dampers are the typical examples in this category.
Motion-activated dampers are secondary devices that absorb structural energy through their motion. They are tuned to resonate with the main structure, but, out-of-phase from it. These dampers absorb the input energy of the structure and dissipate it by introducing extra forces to the structure; therefore, they let less amount of energy to be experienced by the structure.
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2015
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Tuned mass dampers (TMDs) and tuned liquid dampers(TLDs)
are the examples in this category.
Tuned liquid damper types:
Tuned liquid dampers (TLDs) can be implemented as an active or passive device and are divided into two main categories: tuned sloshing dampers (TSD) and tuned liquid column dampers (TLCDs).
TSD: Tuned Sloshing Damper, TLCD: Tuned Liquid Column Damper, LCVA: Liquid Column Vibration Absorbers, DTLCD: Double Tuned Liquid Column Damper, HTLCD: Hybrid Tuned Liquid Column Damper, PTLCD: Pressurized Tuned Liquid Column Damper.
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2015
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Comparison
Type What it do How Main resistance
Structural modifications Resist the additional
straning actions form lateral loads.
By adding stiff elements (e.g.
shear wall, farm element, etc.)
Wind & Ground movement.
Aerodynamic modifications
Avoid the wind or enhancement of
it's behavior.
By making an Aerodynamicshap
e design for the overall building.
Wind.
Base isolation Avoid lateral loads (earth movement
)
By inserting a new elements under the foundations
and adding another
foundation under the base isolation
element.
Ground movement.
Damping Resist and reduce the relative lateral
movement between the
foundations and the super structure.
By adding a mass or a force acting
real time with the shake of the
building.
Wind & Ground movement.
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2015
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Tuned liquid damper
Type Force source Position Advantage T.S.D Water
sloshing force On the top of the building.
suited for small scale excitations
T.L.C.D Variance of mass while liquid motion
On the top or near top.
More advantageous and can be installed anywhere
C.T.L.D Structure & liquid mass
N.A efficiency, but costly
Structural vs Auxiliary:
Structural Auxiliary
Huge mass added. Less mass (about 2% of the hole structure mass )
Adds stiffness to the structure (less structure time period)
No stiffness or very small additional stiffness.
No lateral load force reduction
Reduce up to 50% of the forces.
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2015
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Analytical Models
In this chapter selected models that are considered in this study
are: introduced. Since the liquid behaviour is highly
1- nonlinear, considering nonlinearity of crucial importance
leads to the wave breaking
2-using shallow water in tanks occurrence under various excitation amplitude and frequency combinations where the
liquid surface is no longer continuous.
Therefore, the models presented in this chapter were selected
with the nonlinearity and wave breaking in mind for rectangular
tanks filled slopped bottom shape tanks (Olson and Reed 2001;
Xin et al. 2009
Gardarsson et al. 2001) and introduced models that are able to
account
3- for slopped bottom shapes, one of these models is also
included in this study There are two common approaches that
have been used to model the liquid-tank behaviour. In the first
one the dynamic equations of motion are solved, whereas in the
second approach the properties of the liquid
damper are presented by equivalent mass, stiffness and
damping ratio
essentially modeling the TLD as an equivalent TMD (Tuned Mass
Damper ) .
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2015
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Solving Liquid Equations of Motion
Several researchers have investigated the liquid behaviour
based on solving the liquid equations of motion
. The assumptions they made along with numerical methods
they used to solve the liquid equations of motion have a
significant effect on their prediction. Ohyama and Fujji (1989)
were among the first who introduced a numerical model for the
TLD.
Using among the first who introduced a numerical model for the
TLD .
Using potential flow theory their model was able to take care of
nonlinearity however, computational time was the main
problem with this model (Sun et al. 1992). Kaneko and Ishikawa
(1999) used an integrating scheme to solve continuity and
Navier-Stokes equations without any consideration for wave
breaking. Zang et al. (2000) used a linearized form of Navier -
Stokes equations
. Fediew et al. (1995) assumed that the derivative and higher
orders of the velocity and wave height can be neglected due to
small values of velocity and wave height; however, this
assumption works for weak excitations or when the frequency of
excitation is away from that of
the TLD (Lepelletier and Raichlen 1988). Ramaswamy et al.
(1986) solved nonlinear Navier -Stokes equations using Lagrang
ian description of fluid The model has some physical problems
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2015
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motion and finite element method involving sloshing dynamics
of inviscid and viscous fluids.
Although the amplitude excitations, they assumed a linear
behaviour of the liquid sloshing.
Yamamoto and Kawahara (1999) used arbitrary Lagrangian
Eulerian (ALE) form of Navier -Stokes equations to predict the
liquid motion .
The model tends to be unstable in the case of large amplitude
sloshing.
To solve the instability problem a smoothing factor is
considered and the accuracy is highly dependent to the value of
this factor that varies from zero to one with no clear outline for
the selection.
Siddique and Hamed (2005) presented a new numerical model
to solve Navier -Stokes and continuity equations. Although it is
indicated that the algorithm can accurately predict the sloshing
motion of the liquid under large excitations , the model is unable
to predict the deformations in the case of surface discontinuity
where screen exist or wave breaking occurs. Frandsen (2005)
developed a fully nonlinear 2- D -transformed finite difference
model based on inviscid flow equations in rec tangular tanks.
The model was not able to capture damping effects of liquid and
shallow water wave behaviour.
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2015
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Sun’s Model
Sun et al. (1992) introduced a model to solve nonlinear Navier -
Stokes and continuity equations.
A combination of boundary layer theory and shallow water
wave theory is employed and resulting equations were solved
using numerical methods . An important aspect of this model is
that it considers wave breaking under large excitations by means
of two emprical coefficients. In what follows, a summary of this
model will be provided.
The rigid rectangular tank shown in figure 3. 1 with the length
2𝑎 , width 𝑏
and the undisturbed water level ℎ is subjected to a lateral
displacement 𝑥 𝑠 .
The liquid motion is assumed to develop only in the − plane. It
is also assumed that the liquid is incompressible, irrotational
fluid, and the pressure is constant on the liquid free surface.
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2015
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Figure 3.1: Dimensions of the Rectangular TLD
The continuity and two- dimensional Navier -Stokes equations
that are employed to describe liquid sloshing are defined as
where 𝜕 (𝑥 , 𝑧 , 𝜕 ) and 𝜕 (𝑥 , 𝑧 , 𝜕 ) are the liquid velocities
relative to the tank in
the 𝑥 and 𝑧 direction, respectively, 𝑔 is the gravity
acceleration, 𝑝 is the pressure, 𝜌 denotes the density and 𝑣
represents the kinematic viscosity of the liquid Because of the
relatively small viscosity of the liquid, the friction is only
appreciable in the boundary layers near the solid boundaries of
the tank .
The liquid outside the boundary layers is considered as potential
flow and the velocity potential can be expressed as (Sun 1991)
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2015
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where 𝑘 is wave number and H is defined as (Sun 1991)
Based on the shallow water wave theory, potential is assumed
as (Shimisu and Hayama 1986)
𝛷 (𝑥 , 𝑧 , 𝜕 ) = 𝛷 (𝑥 , 𝜕 ). cosh 𝑘 (ℎ + 𝑧𝑧 ) (4 −
3)
The boundary conditions are described as
𝛷 ( , 𝜕 ) in equation (4- 3) can be determined by the boundary
conditions.
Then, using equation (4- 3) , 𝜕 and its differentials are expressed
in terms of 𝜕 .
Since the liquid depth is shallow, t he governing equations are
integrated with respect to z from bottom to free surface to
obtain :
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2015
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𝑘( = tanh 𝑔𝑇, ) ℎ𝑘( tanh ) / 𝜂+ ℎ( 𝑘= tanh 𝜙 ,) ℎ𝑘( = tanh 𝜎 Where
+ h )
𝜕 and are the independent variables of these equations . 𝜆
in equation (6) is a damping coefficient accounting for the
effects of bottom ,
side wall and free surface, and is determined as (Sun et al.
1989):
In which S stands for a surface contaminating factor and a value
of one corresponding to fully contaminated surface is used in
this model (Sun et. Al 1992). is the fundamental linear sloshing
frequency of the liquid and can be found as (Sun 1991)
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2015
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in equation (6) are employed to account for wave 𝑎𝑑and 𝑓𝐶
breaking when ( 𝜂 > ℎ ). These coefficients are initially equal to a
unit value, and when wave breaking occurs, takes a constant
𝑎𝑑𝐶value equal to 1.05 as suggested by Sun et al. (1992).
depends on 𝑚𝑎𝑥 that is the maximum displacement
experienced by the structure at the location of the TLD, when
there is no TLD attached; and it can be found as
Equations (5) and (6) are discretized in space by finite difference
method
and solved simultaneously using Runge- Kutta-Gill method to
find u and η.
Knowing η the force introduced at the walls of the TLD can be
described
as [29]:
are the free surface elevations at the right and 0𝜂and 𝑛𝜂where
left tank walls, respectively.
To consider TLD -Structure interaction, a single- degree-of-
freedom
(SDOF) structure with TLD is considered as shown in figure 3.2.
The
equation of motion of the TLD -structure system subjected to a
ground
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2015
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) is 𝑔𝑎acceleration (
are structural mass, damping 𝑠wand 𝑠𝜉, 𝑠𝑘, 𝑠𝑐, 𝑠𝑚where
stiffness, damping ratio and natural frequency coefficient,
structural relative displacement to represents 𝑠𝑥respectively,
displacement experienced the ground which is meanwhile the
is ground acceleration and F is TLD base shear 𝑔𝑎, by the TLD
due to sloshing force on the TLD wall that is given by equation
(10).
Equations (5), (6) and (12) must be solved simultaneously in
order to fin d the response of the SDOF structure equipped with
TLD. A step-by-step procedure is employed where knowing the
structural acceleration at each
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2015
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Figure 3.2: Schematic of SDOF System with a TLD Attached to It
step, equations (5) and (6) are solved using Runge- Kutta-Gill
method and F calculated on Then, F, SDOF is
calculated using Runge- Kutta-Gill method from equation (12)
and next step acceleration is found to be used in the next step
calculations.
Appendix A provides information on the discretization technique
and application of Runge-Kutta-Gill method.
Equivalent TMD Models
Another approach to investigate TLD behaviour is replacing the
TLD by its equivalent TMD and finding the effective TMD
properties such as stiffness , damping ratio , and mass that can
properly describe TLD characteristics.
These equivalent properties are found through experimental
procedures.
Sun et al. (1995) found equivalent TMD properties base on
nonlinear
Navier-Stokes equations and shallow water wave theory.
However, the experimental cases presented in this study are
limited.
Casciati et al. (2003) proposed a linear model which can
interpret frustum -conical TLDs behaviour for small. The
excitations model is not able to capture high amplitude
excitations and instability problems occur near resonance.
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2015
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Tait(2008) developed an equivalent linear mechanical model
that acc ounts for the energy dissipated by the damping screens
for both sinusoidal and random excitation.
Yu’s Model.
Yu (1997) and Yu et al. (1999) modeled the TLD as a solid mass
damper that can capture nonlinear stiffness and damping of the
liquid motion.
This mechanical model can capture the behaviour of the TLD in a
broad range of excitation amplitudes and can be a good TLD
design tool. An equivalent Nonlinear-Stiffness-Damping (NSD)
model is proposed through an energy matching procedure when
the dissipated energy by the equivalent NSD model is matched
by that of the TLD. Figure 3.3 shows the schematic of the
characterized SDOF model of the TLD; , 𝑐𝑑 , and 𝑚𝑑 refer to
the stiffness, damping coefficient , and mass of the NSD model,
respectively. A challenge in this model is the determination of
the NSD parameters to describe TLD behavior.
As it is shown in figure 3.3, the NSD model used in simulation is
based on introducing the interaction force made by liquid
sloshing inside the tank. Considering t he TLD as an equivalent
linear system, this force can be characterized by its amplitude
and phase.
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Energy dissipation per cycle is found by equation (13) and non-
Energy dissipation per cycle is found by equation (13) and non-
dimensionalized version is provided as equation (14).
Where, shows integration over the shaking table displacement
per cycle, 𝐹𝜕 is the force generated by the liquid sloshing
motion in the tank , 𝑚𝜕 refers to the mass of the liquid, w is the
excitation angular frequency of
Figure 3.3: Schematic of the a) TLD and b) Equivalent NSD Model
the shaking table (equation (8)), A is the amplitude of the
sinusoidal excitation and the denominator of (14) is the
maximum kinetic energy of the water mass treated as a solid
𝑑𝐸he NSD model dimensional energy dissipation of t-mass. Non
is determined based on NSD model behaviour when it is
subjected to harmonic base excitation with frequency ratio β.
The non-dimensionalized amplitude and phase 𝜙 that describe
the interaction force of the NSD model and are
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2015
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calculated as :
is the 𝑒𝑓⁄ is the excitation frequency ratio, 𝑑𝑓𝑒𝑓where =
excitation frequency is the natural frequency of the NSD,
frequency dissipation range of -over high w 𝐸is fitted to 𝑑𝐸
the frequency using least -squares method. In this procedure 𝑚𝑑
, the stiffness 𝑑𝑓and w𝑓 𝜉initial values for = , and assuming
and damping coefficients are determined .
The results are analyzed through two ratios; the first is
frequency shift ratio as defined by:
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2015
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stands for the linear fundamental frequency of the w𝑓where
liquid and is defined as :
where h is the undisturbed height of the water and a is the half
length of the tank. The second ratio is the stiffness hardening
ratio that is defined
The above matching scheme is applied to a set of experimental
tests in order to evaluate the equivalent stiffness and damping
ratio for the NSD model. The equivalent stiffness and damping
ratio are investigated as a function of the wave height, water
depth, amplitude of excitation and the tank size. Non-
dimensional value of the amplitude was found to be the most
suitable parameter to describe the stiffness and damping ratio.
This value is described as:
where 𝑤𝑤 is the amplitude of excitation and a is the half length
of the tank in the direction of motion . To calculate , as it is
shown in figure 3. 4, each time the displacement curve crosses
the time axis , the maximum displacement during the previous
half cycle x max, i-1 is calculated and the absolute value of that
is considered as 𝑤 for the its half cycle in order to find ᴧ .
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2015
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Figure 3.4: Displacement Time History to Calculate
After finding the corresponding values of and κ from
equations (18) and (20), they are plotted versus ᴧ and the best-
fitted curve is found in order to find the equations for damping
ratio and stiffness hardening ratio.
Yu (1997) and Yu et al. (1999) obtained the damping ratio as
As stiffness hardening ratio changes considerably before ᴧ =
0.03 (corresponding to weak wave breaking) and then starts to
grow up sharply after ᴧ = 0.03 (corresponding to strong wave
breaking), Yu (1997) and Yu et al. (1999) obtained the equation
for 𝜅𝜅 is obtained as
Finally, as it is shown in figure 3 .5, a two -degree-of-freedom
model is considered to investigate the interaction of TLD -
structure system when a TLD is attached to a SDOF structure. In
this model in equation (21) is found from the structural
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2015
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displacement where the TLD is attached (usually top floor). So,
each time the displacement curve crosses zero axis stiffness and
damping ratio of the NSD model are updated based on
equations (22), (23) and (24) corresponding to the top structural
displacement. Figure 3.6 illustrates the schematic for stiffness
and damping parameter updating of the NSD model. The
equations of motion are presented in matrix form as
are the mass, damping, 𝑠 𝑥and 𝑠 𝑥, 𝑠𝑥, 𝑠𝑘, 𝑠𝑐, 𝑠𝑚where
stiffness, relative displacement, velocity and acceleration of the
structure , respectively. The same parameters with the
, 𝑠𝑐, 𝑑𝑚parameters , subscripts d refer to the NSD model. The
are assumed to be given in this procedure. 𝑠𝑘and
Figure 3.5: 2-DOF System: a) Structure with TLD b) Structure with
NSD Model
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2015
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Figure 3.6: Schematic for Determining the NSD Parameters
𝑑𝑚, 𝑠𝑐, 𝑠𝑘Given Constants: ,
Sloped Bottom Models
There are studies on the effect of changing the tank bottom
shape from rectangular to sloped bottom pattern. Gardarsson
et al. (2001 ) investigated the performance of a sloped- bottom
TLD with an angle of 30° the tank base. It is observed that more
liquid mass participates in to sloshing force in the slopped-
bottom case leading to more energy dissipation. Olson and Reed
(2001) investigated the sloped- bottom TLDs el developed by
using non-linear stiffness and damping mod Yu (1999) . It is
shown that the sloped- bottom tank should be tuned slightly
higher than the fundamental frequency of the structure to
introduce the most effective damping. Tait and Deng (2009)
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showed that the normalized effective mass ratio for a sloped-
bottom tank with a sloping angle of 20° is larger than the
normalized effective mass ratio of flat-bottom tanks .
Xin’s Model
Xin (2006) and Xin et al. (2009) proposed a model that is capable
to investigate sloping - bottom TLD based on the linearized
shallow water wave equation ( Gardarsson 1997), using the
velocity potential function and wave height equation suggested
by Wang (1996) and liquid damping introduced by Sun et al.
(1995) and Sun (1991). As it is shown in figure an equivalent flat
- bottom TLD model is proposed to simulate the the sloped-
bottom case and the equivalent flat -bottom tank is kept equal
𝐿 ′ of the equivalent flat-bottom tank is equal to the total length
of the sloping bottom).
The maximum water depth H' remains the same when the
equivalent width of the flat - bottom tank 𝐵 ′ is decreased in
of the sloshing water the w𝑉to keep the total volume order
same as that of the sloped-bottom tank . 𝐵 ′ is defined as (Xin
2006):
floor of the ℎ𝑗 ) applied to the t( 𝑗𝐹The horizontal control force
building structure by a sloping - bottom TLD is equal to the
resultant of the fluid dynamic pressures on the left and right
walls of the flat - bottom TLD tank ; and is expressed as (Xin et
al. 2009)
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Figure 3.7: Equivalent Flat-Bottom Tank
) represents the relative t( 𝑗 𝑋is the water density, 𝜌where
building floor with respect to the base of ℎ𝑗the acceleration on
t the base the ground acceleration a ) refers tot( 𝑔𝑥the building,
of the building, and 𝑦 (t ) is the first modal acceleration of water
sloshing. The modal response of water
sloshing can be determined as :
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Where M , C , and K are the mass, damping coefficient, and
stiffness matrices of the structure ;
𝑋 , 𝑋 , and 𝑋'' represent the relative acceleration , velocity, and
displacement vectors with respect to the base of the building ; I
is the earthquake influence vector with unity for all elements;
is the TLD influence vector with zero elements except 𝑓I and
floor of the building ℎt𝑗he element corresponding to the for t
where the TLD is attached that is unity. Knowing the initial
condition, equation (28) is solved and the tank acceleration is
calculated and used in equation (27) to find the interface force.
Having the interface force and using equation (31) structural
displacement and acceleration are found for next step
calculations.
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In this study, since the experiments were done for a rectangular
tank , these equations are solved for the equivalent rectangular
tank in order to investigate this model’s accuracy. The Simulink
used to solve these equations is presented in Appendix B
Experimental Results and Analysis
Testing Method
In this study the real-time hybrid Pseudodynamic (PSD) testing
method has been employed to investigate the TLD behaviour
under a range of structural parameters and load cases.Hybrid
PSD testing method combines computer simulation with
physical by testing part of the structure physically (experimental
substructure) coupled with a numerical model of the remainder
of the structure (analytical substructure )
When the experimental substructure has load rate dependent
vibration characteristics as in the case of TLD, the hybrid PSD
test needs to be performed dynamically in real - time. By
employing real - time hybrid PSD interaction has been
investigated by test in this study, the structure- TLD only
physically testing the TLD as the experimental substructure and
a wide range of TLD - structure system properties were easily
investigated by modifying the parameters of the structure as the
analytical substructure As it is shown in figure 4.1 , the whole
system is divided into the experimental (TLD) and analytical
(structure) substructures . TLD is tested physically and the
interaction force is measured using a load cell. The response of
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the structure considering also the measured interaction force
from the TLD under the specified external loading is calculated
numerically using Simulink and Real -time Workshop. In this
study the analytical substructure is modeled as a single degree
of freedom oscillator. The displacement command generated by
the Simulink model is imposed on the shaker. The
software/hardware communication and synchronization issues
are taken care of by using the WinCon/Simulink interface.
Figure 4.1: Schematic of the Hybrid Testing Method
Test Setup
Figure 4.2 shows a picture of the test setup. The shaker table
consists of a 1 Hp brushless servo motor driving a 12.7 mm lead
screw. The lead screw drives a circulating ball nut which is
coupled to the 457x457 mm table. The table itself slides on low
friction linear ball bearings on 2 ground hardened shafts and has
76.2 mm stroke. The shaker comes with WinCon software, the
real-time control software that runs Simulink models in real -
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time. The built-in control laws are able to impose harmonic or
preset earthquake historical data under displacement control. In
this study a velocity feed forward component was added to
improve the tracking of the command displacements by the
shaker. The load cell is a 22.2 N ( 5 lb) load cell that can carry
compression and tension loads. The tank is made of plexi-glass
that has dimensions of 464 mm (length), 305 mm (width). A
water height of 40 mm which corresponds to 0.667 Hz of
sloshing frequency of the tank (based on equation (8)) was
selected there the weight of the TLD was 5.64 kg.
Figure 4.2: Experimental Setup
As it is shown in figures 4.1 and 4.2, the tank is placed on
greased ball bearings to eliminate friction. Special attention was
given to keep the tank in the perfectly horizontal position. Only
a few degrees out of horizontal position was observed to
introduce large amount of error in the measured restoring force.
Two rollers are also placed at the two sides of the tank in order
to keep its movement in one direction.
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TLD Subjected to Predefined Displacement
History
This section summarizes the results where the TLD was
subjected to displacement histories with amplitude of 20 mm
and various frequencies to cover a range of β from 0.5 to 1.5.
The frequency ratio β , as previously defined, is the ratio of the
frequency of loading to the sloshing frequency of the tank. By
considering the energy dissipated in each case (see figure 4.3),
the effective value for β was obtained. As can be seen in figure
4.3 energy dissipated by the TLD increases until β <1.2, and
starts to decrease for values of β >1.2, rendering β =1.2 as the
effective frequency in terms of energy dissipation. To shed some
light into the TLD energy dissipation behavior, another set of
experiments were performed. In these tests, the water inside
the TLD was replaced with an equivalent solid mass while the
TLD was imposed to the same predefined displacement
histories. The measured restoring forces in these tests
correspond to the inertia component of the interface force. By
subtracting the inertia component from the interface force, the
sloshing force was calculated for each frequency ratio. Figure
4.4a shows the inertia and sloshing force components of the
interface force for β=1.5.
It can be seen that these component s have a destructive
interface where they almost cancel each other resulting in very
little if not nonexistent
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energy dissipation for this frequency (see figure 4.3). As it is
shown in figure 4.4b for β =1.2, on the other hand, the inertia
and sloshing force components have constructive interface
leading to an efficient energy dissipation as described earlier.
Figure 4.4a: Destructive Interface of Sloshing and Inertia Forces
at 𝛽𝛽 = 1.5
Figure 4.4b: Constructive Interface of Sloshing and Inertia Forces
at 𝛽𝛽 = 1.2
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TLD-Structure Subjected to Sinusoidal Force
In this section, using real -time hybrid PSD method, the TLD -
structure system was investigated under a series of sinusoidal
force. To be able to three different force observe weak and
strong wave breaking behavior amplitudes (i.e., 3 N, 5 N, and 8
N) were used while the forcing frequency adjusted to be the
same as the structural frequency (see table 4.1). In addition to
the forcing function amplitude, a range of structure to TLD
sloshing frequency ratio ( α ) from 0.5 to 1.5 was considered in
the hybrid simulations. The TLD properties were kept
unchanged; to obtain the aforementioned range of α , the
structural stiffness in the analytical the structure and the
substructure was adjusted. The mass of structural
Table 4.1: Parameters for experiments introduced in Chapter 4.4
Structural displacements in the form of deformations relate to
the damage of the structural members during seismic events. On
the other hand nonstructural components (ceiling - wall
attachments , experience considerable inertial forces due to
floor accelerations
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Figure4.5 present the displacement/ acceleration versus
frequency response graphs for 3 different force levels
considering the structure with and without the TLD.
Figure 4.5: Structural Displacement and Acceleration with and
Without TLD
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Figure 4.6 represents the data from figure 4.5 in terms of
percent reductions of displacements and accelerations. From
these figures it can be concluded that, for the forcing levels
considered corresponding to weak and strong wave breaking,
TLD is remarkably efficient in reducing the displacement and
acceleration response around the frequency ratio α near
Figure 4.6: Structural Displacement and Acceleration Reduction
one, where the tank is in resonance with the structure. The
results from the experiments with the sinusoidal forcing
function were also used to investigate the accuracy of the
models that were selected and presented in chapter 3. In each
case, the error between the experiment and model prediction
was quantified by:
represents 𝑝𝐹stands for measured values and 𝑚𝐹where
predicted values from the models.
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Figure 4.7: Comparison Between Experimental Results and
Analytical Predictions for 𝐹 = 3𝑁
Figure 4.7 presents the comparison between experiment and
numerical model predictions for the force level of = 3𝑁𝑁 Since
no wave breaking was observed, all the models were able to
capture the TLD behavior reasonable well. Considering the
entire range of α , the error quantified by equation (32) for Sun’s
and Xin’s models is around 2cm, and for Yu’s model it is 2.7 cm.
For the range of 𝛼𝛼 between 0.9 and 1.1, which is the range
where TLDs are tuned in the design practice, Yu’s and Xin’s
model
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introduce more accurate predictions with 0.7 and 0.6 cm error
while Sun’s model has 1.8 cm error in this range.
Figure 4.8: Comparison Between Experimental Results and
Analytical Predictions for 𝐹 = 5𝑁
In the case of = 5𝑁𝑁 , where some wave braking near 𝛼𝛼 = 1
occurs, Yu’s and Xin’s models have a good prediction while Sun’s
model overestimates the displacement. For α smaller than 0.8
the models do not agree well with experimental results while
for α larger than 1.3 Sun’s model agrees well with experimental
results and Xin’s model overestimates the displacement.
Although Sun’s model has accounted for wave breaking in its
formulation, it is unable accurately liquid for values near one
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where some wave breaking is observed. Overall Xin’s model
generates more accurate results with 3 cm error in comparison
with Yu’s and Sun’s model with about 4.5 cm error. For
between 0.9 and 1.1, Yu’s and Xin’s model accumulate an error
of 0.8 and 0.6 cm, respectively; whereas Sun’s model has less
accurate predictions with 3.7 cm error.
Figure 4.9: Comparison Between Experimental Results and
Analytical Predictions for 𝐹 = 8𝑁
For = 8𝑁𝑁 , where wave breaking was captured during almost
all frequency ratios, the accuracy of all the models suffer.
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Sun’s model overestimates the structural displacement for the
entire range of the frequency ratio. For α near one, Yu’s and
Xin’s models seem to match well with experiment results and
Yu’s model continues to have a good agreement with
experiment for α larger than one. Overall, Yu’s and Xin’s model
show more accurate results with 7 cm error and Sun’s model has
a less accurate prediction with an accumulated error of 8.5 cm.
For between 0.9 and 1.1, Xin presents a more accurate model
with 1.5 cm error in comparison with Yu’s and Sun’s model with
3 and 6 cm error, respectively. Considering all three load cases
and the ranges of the frequency ratios , Yu’s model provides
reasonable predictions in both weak and strong wave breaking
and in a broad range of frequency ratios. Xin’s model presents
good results near 𝛼 = 1 and overestimates the displacement for
α larger than 1.2. Sun’s model can predict the TLD behaviour in
the absence of wave breaking, i.e. 𝐹 = 3 , however
overestimates the displacements in the case of wave breaking.
Mass Ratio
The TLD efficiency under a range of mass ratios (the ratio of the
mass of water to that of the structure) has been investigated in
terms of structural displacement and acceleration reduction.
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Table 4.2: Parameters for Experiments Introduced in Chapter 4.5
As it is shown in table 4.2, t he structural stiffness, mass and
damping coefficient were changed in order to capture different
mass ratios varying from 0.5% to 5% while the damping ratio
remains constant as well as the structural frequency which is
equal to the tank and forcing frequency. The amplitude of the
applied sinusoidal force has been also changed in a way to reach
to the same steady state amplitude in the absence of TLD.
Figure 4.10: The Effect of Mass Ratio on TLD-Structure Behaviour
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Figure 4.11: Acceleration and Displacement Reduction for
Different Mass Ratios
It can be seen from figure 4.10 and 4.11 that the efficiency in
reducing the displacements and accelerations increase as the
mass ratio increases up to 3%. For larger mass ratios (i.e., up to 5
%), although the response of the structure with TLD is reduced in
comparison to the structure without TLD (see figure 4.10), there
is a reduction in the efficiency in comparison to the TLD’s with
mass ratio less than 3% (see figure 4.11). Noting that the
increasing the mass ratio from 1.5% to 3% increases the
efficiency in displacement acceleration reduction only by 10%
while considerably practical point of view 1.5% mass ratio can be
recommended as the optimum value.
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Figure 4.12a: Displacement Increase Due to Undesirable TLD
Forces for 5% Mass Ratio
Figure 4.12b: Displacement Time History for 3% Mass ratio
Another interesting phenomenon that was observed for the
mass ratio of5% was beating (see figure 4.12). Kareem and Yalla
(2000) concluded that the off -diagonal mass terms in the
coupled mass matrix of the damper-structure system was
responsible for this phenomenon.
Figure4.12b shows the TLD displacement in the absence of
beating.
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Structural Damping
Ratio
The effect of structural damping ratio on the TLD behaviour is
investigated here. Damping ratio was varied from 0.2% to 5% as
the typical range of damping for building structures.
Table 4.3: Parameters for Experiments Introduced in Chapter 4.6
As it is shown in Table 4.3, structural mass and stiffness w ere
kept constant in order to have the structural frequency constant
and equal to the tank and forcing frequency. The force
amplitude had constant amplitude equal to 9 N during all tests.
In figure 4.13, as the structural damping ration increases the
effectiveness of TLD in reducing the structural displacements
decreases. For the case considered, when the structure has 5%
inherent damping, its displacement response with and without
TLD is almost the same. It may be because, when the structural
damping is already high, the TLD - structure system does not go
through large displacements, where TLD does not get the chance
to dissipate energy.
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Figure 4.13: The Effect of Damping Ratio on TLD-Structure
Behaviour
In the case of acceleration, for the case considered, an increase
in the accelerations for the system with TLD was observed for
structural damping ratios more than 0.015. Therefore, it can be
concluded that TLD is more effective for structures with low
damping ratios. As the structural damping ratio increases TLD
not only ceases to become effective in reducing the
displacements, it can also amplify structural accelerations (see
figure 4.14). It needs to be pointed out that to establish
boundaries for the effective damping ratio ranges; an extensive
study with different force levels is required
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Figure 4.14: Acceleration and Displacement Reduction for
Different Damping Ratios
TLD-Structure Subjected to Ground Motions
Here the TLD-structure system is subjected to three well known
ground motions. The effectiveness of TLD and the accuracy of
the selected models in predicting the response under seismic
loading are investigated. El Centro, Kobe and Northridge
earthquakes have been used and due to the shaking table
displacement limitations, each record was scaled down by 0.3,
0.1 and 0.05 factors, respectively.
As can be seen in figures 4.15 to 4.17, the TLD is quite
effective in acceleration. However, it is noted that it takes a
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while for TLD to take effect (for the liquid to be set in motion
and dissipate energy) and the first peak displacement of the
time history remain unaffected by the existence of TLD for all
three earthquakes. This is expected as TLDs have been
considered ineffective under impulse type sudden loading
(Xin2009).
4.15: Structural Response with and Without TLD under El Centro
Earthquake
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4.16: Structural Response with and Without TLD under Kobe
Earthquake
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4.17: Structural Response with and Without TLD under
Northridge Earthquake
Additionally the accuracy of the selected models to predict TLD -
structure response under seismic loading was investigated and
shown in figures4.18 to 4.26. As it is shown in figure 4.18 to
4.20, Sun’s model prediction for Northridge ground motion
matches well with experimental results.
In the case of El Centro and Kobe ground motions Sun’s model
overestimates the displacements, but the model has a
reasonable prediction of the accelerations.
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4.18: Hybrid Test Results and Sun’s Model Predictions under El
Centro Earthquake
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4.19: Hybrid Test Results and Sun’s Model Predictions under
Kobe Earthquake
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4.20: Hybrid Test Results and Sun’s Model Predictions under
Northridge Earthquake
Figure 4.21 to 4.23 indicate that, although on the conservative
side, Yu’s model have a better agreement (less error) compared
to the other two models under seismic loading. Also, the
acceleration of Yu’s model agrees very well with the real-time
hybrid test results.
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4.21: Hybrid Test Results and Yu’s Model Predictions under El
Centro Earthquake
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4.22: Hybrid Test Results and Sun’s Model Predictions under
Kobe Earthquake
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4.23: Hybrid Test Results and Yu’s Model Predictions under
Northridge Earthquake
As can be seen from figures 4.24 to 4.26, Xin’s model is the least
accurate among the three selected models in predicting the
response under seismic loading. The displacement comparison
between Xin’s model and the real - time hybrid test result
reveals that this model underestimates the displacements in the
earlier times of the time history followed by overestimation.
Phase and amplitude inaccuracy in both displacement and
acceleration comparisons are apparent.
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4.24: Hybrid Test Results and Xin’s Model Predictions under El
Centro Earthquake
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4.25 :Hybrid Test Results and Xin’s Model Predictions under
Kobe Earthquake
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4.26 :Hybrid Test Results and Xin’s Model Predictions under
Northridge Earthquake
Investigating the accuracy of the three selected models in
comparison to the real -time hybrid testing results, Yu’s model
was found to be more accurate model in both displacement and
acceleration prediction. Sun’s model has also reasonable enough
answers especially in the case of low amplitude ground
accelerations and Xin’s model has the least accuracy among the
three models under seismic loading.
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Case of Study And Advantages
1. From this study, it has been found that the TLD can be
successfully used to control vibration of the structure.
2. The TLD is found to be more effective, when it is placed at the
top storey of the structure. In the study to access the effect of
TLD in structural damping placed at various floors, it has been
found that the amplitude of displacement at 10th storey of the
structure is 0.35mtr when the TLD is placed at the 10th storey,
which increases to 0.6mtr when TLD is placed at 5th floor. The
loading applied on the structure is sinusoidal loading at
resonance condition to fundamental frequency of the structure .
3. A study has been done to found the effect of mistuning of the
damper in damping effect of TLD. It has been found that, TLD is
most effective when it is tuned to the fundamental natural
frequency of structure. Under tuning or over tuning of TLD to
fundamental natural frequency of structure puts adverse
effect on the damping of the TLD. In the study to access the
effect of mistuning of TLD in structural damping, it has been
found that the amplitude of displacement at 10th storey of the
structure is 0.35mtr when the TLD is placed at the 10th storey,
which increases to 0.45mtr when TLD is both under tuned and
over tuned to 95.10% and 105.13% of fundamental natural
frequency of structure respectively
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TLD was most effective when the structure was excited at
resonance frequency of the structure, reducing the ratio
from 22 to 4 (80% reduction in vibration).
Case study
For the applications carried out in the scope of this paper, and
having in mind a specific building, the ground motion considered
was defined only along one horizontal direction. The building
chosen for this study is representative of the modern Portuguese
architecture and was designed and built in the 1950s, when
earthquake design was not contemplated in the national
standards. This building has nine-storeys. The option for this
case-study is justified by the moderate to high local seismic
hazard of the Lisbon region and by the significant number of
buildings with this typology designed and built in Southern
European cities in that period.
The block plan is rectangular with 11.10m width and 47.40m
length. The building has the height of 8 habitation storeys plus
the pilotis height at the ground floor. The “free plan” is also a
reference because the house was conceived in a way of
flexibility in use. But, the 12 structural plane frames define the
architectural plan of the floor type, with 6 duplex apartments.
The distance between frame’s axes is 3.80m. Each frame is
supported by two columns and has one cantilever beam on each
side with 2.80m span, resulting in 13 modules.
The building geometry and dimensions of the RC elements and
infill walls were given in the original project (1950–1956), and
were confirmed in the technical. The structure is mainly
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composed by twelve plane frames oriented in the transversal
direction (direction Y, as represented in Fig. 2).
The twelve transversal plane frames have the same geometric
characteristics for all beams and columns. A peculiar structural
characteristic of the type of buildings, with direct influence in
the global structural behaviour, is the ground storey without
infill masonry walls. Furthermore, at the ground storey the
columns are 5.5m height. All the upper storeys have an inter-
storey height of 3.0m. A detailed definition of the existing infill
panels were considered in the structural models.
For the numerical analyses, constant vertical loads distributed
on beams were considered in order to simulate the dead load of
the self-weight including RC elements, and infill walls, finishing,
and the correspondent quasi-permanent value of the live loads,
.20kN/m.totalising a value of 8
Fig. 2 Case study: a general views of the building block under
analyses; b structural system (plan)
The mass of the structure was assumed concentrated at storey
levels. Each storey has a mass, including the self-weight of the
structure, infill walls and finishings, and the quasipermanent
value of the live loads, of about 4M tons. For the dynamic
analysis, the storey mass is assumed to be uniformly distributed
on the floors
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Design of a TLD for the case study
The procedure adopted for the design of the tuned liquid
dampers for the studied building was as follows. The procedure
adopted for the design of the tuned liquid dampers for the
studied building was as follows. From previous analysis
(Rodrigues et al. 2010), it was found that the most flexible
direction of the building corresponds to the longitudinal
direction. Also, in this case study, the absence of infill’s in the
ground story induces a dynamic behaviour mainly governed by
the first mode. In this numerical analysis, intending to show the
efficiency of the TLDs in the seismic protection of building
structures, it was considered the design of the TLDs only
relatively to the longitudinal direction and ignoring the upper
modes influence. However, it is recalled that, in most building
structures, the influence of various modes should be taken in to
account.
The building first natural frequency in the longitudinal
direction measured in-situ (Rodrigues et al. 2010) was f = 1.08Hz.
The sloshing frequency of the fluid is equalled to the first natural
frequency of the building:
where T is the natural period of the structure and ω is the
corresponding angular frequency.
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In terms of linear frequency (in Hz) the equation of sloshing
frequency of the fluid (Eq. 3), can be rewritten as follows
, and the ,fh Imposing a ratio between the height of the fluid,
length of the tank, L, equal to 0.15, as suggested by Fujino et al.
(1992), and substituting the values for the structure under
analysis in Eq. (5), the following non-linear system of equations
. Land fhcan be obtained as a function of
0441m..0= fh 3000m and.0= L Therefore, on the present case,
In the scope of this work, it was assumed that the width b of the
TLD is equal to its length
L, leading to a quadrangular geometry in plan. This geometry
guarantees that the TLD will behave equally on both horizontal
directions, as opposed to a rectangular tank. From the literature
review, no rule or proposal was found for the height limitation
of the TLDs.
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Summary And Conclusions
- Current trends in construction industry demands taller and
lighter structures, which are also more flexible and having quite
low damping value. This increases failure possibilities and also,
problems from serviceability point of view. Several techniques
are available today to minimize the vibration of the structure,
out of which concept of using of TLD is a newer one. This study is
made to study the effectiveness of using TLD for controlling
vibration of structure.
- In this study a series of experiments have been conducted with
a TLD to investigate the effects of some of the design
parameters of the TLD structure system and also to check the
accuracy of selected models in predicting TLD response. These
models have been compared against experimental data when
they were first published. Unlike these
studies which provided the comparisons for only a few selected
cases, this study considers a broad range of frequency ration,
load amplitude and types; which also enabled the investigation
for determination of effective frequency ratio, mass ratio, and
structural damping ratio. A part of the experiments were
conducted by imposing predefined sinusoidal displacements to
the TLD by using a shake table. The TLD -structure interaction
was investigated by employing real-time hybrid PSD testing
method where the structure was modeled analytically and the
TLD was tested physically in coupled experiment -simulation
mode Frequency Ratio. Subjecting the TLD to predefined
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displacement with various frequencies, it is observ ed that to
design an effective TLD, the ratio of the structural frequency to
that of the TLD should be between 1 and 1.2 when larger
frequency ratios frequency ratios, as the inertia and sloshing
large amount of energy dissipation can be obtained . For
analytical
components of the TLD interface force start canceling each
other, the TLD was observed to be ineffective in dissipating the
energy.
- In the case of three ground motions consider ed (El Centro,
Kobe and Northridge), Yu was observed to be more accurate in
both displacement and acceleration predictions. Having some
overestimations, Sun’s model had also reasonable enough
predictions especially in the case of low amplitude ground
accelerations and Xin’s model predict ed structural response
with some inaccuracy in the response amplitude and phase.
From the results of this study, it can be con cluded that properly
designed TLD is an effective damper to reduce both structural
displacement and acceleration in the case of ground
accelerations and harmonic loads. It is also economical in
comparison with other common kind of dampers. Investigating
the analytical models, it can be concluded that more accurate
models that are able to have a better consideration for wave
breaking occurrence during high amplitude of excitations are
required. Also a more comprehensive experimental/analytical
study is necessary to understand the behavior of TLD under
higher mode and structural nonlinearity effects.
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FURTHER SCOPE FOR STUDY:
1. Both the structure and Damper model considered in this study are linear one; this provides a further scope to study this problem using a nonlinear model for liquid as well as for structure. 2. The structure and Damper model considered here is two-dimensional, which can be further studied to include 3-dimensional structure model as well as damper liquid model. 3. Response of Liquid model can be studied by Mess free methods. 4. This study can be done by introducing obstacles like baffles, screens and floating particles, and the change efficiency in the TLD model can be compared. 5. Further scope, also includes studying the possibility of
constructing Active TLD using controllable baffles and screens.
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Introduction Seismic isolation and energy dissipation technologies have found an
increasing number of applications over the last decade and
particularly over the last few years. The increase in the use of these
technologies may be attributed to the development of analysis and
design guidelines and specifications and the availability of computer
programs for dynamic analysis.
So that in our research we will discuss one of these analysis.
We used models made us able to investigate the liquid motion
behavior, effective range and important TLD parameters through the
El Centro Earthquake .
El Centro Earthquake
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↳ By considering the behavior of two identical points on the two
model structures we managed to have some relations with time
such as displacement and acceleration as shown.
Displacement is decreased dramatically in the case of using T.L.D
as predicted but what about the acceleration? Let us see ..
Displacement-time relationship
relationship
relationshiprelationshiprelationshipre
lationshiprelationship
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As we can see the acceleration is also effected slightly .
Acceleration-time relationship
relationship
relationshiprelationshiprelationshipre
lationshiprelationship
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After that we tried another model to work with, a new structure
with more degrees of freedom.
We used 5 identical structures except of the T.L.D's
Model shape
Deformed shape
1 2 3 4 5
1 2 3 4 5
Case 1: no T.L.D.
Case 2: 1 T.L.D in the last floor.
Case 3: 5 T.L.D s alternately.
Case 4: 2 T.L.D s in the last floor
and in the medial.
Case 5: T.L.D s in all floors.
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And the same with the S.D.F we got out some relations as the
following.
displacement-time relations:
`
Case1 VS Case2
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Conclusion - The acceleration is reduced but not as greatly as the
displacement did.
- The displacement in the M.D.F is effected more than the
S.D.F.
- Adding more T.L.D s in the structure doesn't give us the result
we hoped and it may make the system less efficiency just like
case5 when we used T.L.D s all over the structure.
- The availability of combining another lateral load resisting
system because the T.L.D does not required any special base
treatment or floor constructions.
- When using T.L.D on the M.D.F systems we can get a benefit
in the response with is the decay of the motion faster with
the earthquake age.
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References
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