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Elastic and Inelastic Response of Structural Systems in Seismic Pounding

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Received 15 February 2016; accepted 26 February 2016; published 29 February 2016

1. Introduction

Structural pounding of buildings and bridges during seismic excitations is a well observed phenomenon in the recent past. During Alaska earthquake (1964), it has reported that the tower of Anchorage Westward hotel was damaged by pounding action against the three-storey ballroom portion of the hotel [1] . In the San Fernando earthquake (1971) of severe intensity, it has observed that the second storey of Olive View hospital struck against the stair-tower block, and in addition the first floor of the hospital hit against adjacent warehouse [2] . The survey performed by Rosenblueth and Meli [3] after the earthquake that struck Mexico City in 1985 revealed that pounding was a major factor for structural damages in over 3% - 4.5% of the 330 collapsed or severely damaged buildings under survey, and 15% of all cases suffer major damages. This single earthquake gives a momentum for understanding and studying this particular problem of pounding, which ultimately results in gaining a more research contribution on pounding problem in the latter years after 1988.

Although the pounding is a very complex phenomenon, which escorts several doubts in its numerical modeling, in the recent years this problem is extensively studied by applying various structural modes and using different models of collisions. The preliminary studies of pounding carried out by many researchers in the earlier days before the arrival of powerful softwares were done on lumped mass models. The fundamental study on seismic pounding between the adjacent buildings in series was performed by Anagnostopoulus [4] , where the structures were modeled as single-degree-of-freedom (SDOF) system and collisions were simulated by using linear viscoelastic gap elements. A parametric investigation was conducted and it showed that the end structures experience severer response than interior structures of the series.

Pentelides and Ma [5] have studied the dynamic behavior of damped SDOF elastic and inelastic structures subjected to one-side pounding incidences during an applied ground excitation; the pounding forces are simulated by considering Hertz contact gap element. The effects of gap distance and inelastic structural behavior on the magnitude of pounding forces were evaluated in the published paper. Davis [6] has conducted a numerical investigation on damped SDOF structure impacting against a rigid barrier. Jankowski [7] has presented impact force response spectrum for two adjacent structures, in which pounding force has plotted as an ordinate against the structural vibration period along abscissa.

Maison and Kasai [8] have studied the response of light high rise MDOF building colliding against the massive low rise structures; the pounding forces were calculated only at the top of low rise structures, where it was connected with the adjoining structures by means of linear spring; and in other location of low rise structures no springs were put. Various analytical models based on contact force mechanism and steromechanical mechanism considered for the seismic pounding response of adjacent structures were studied by Muthukumar and DesRoches [9] . The results presented were established for two degrees of freedom linear oscillator to determine the effect of impact modeling strategy, system period ratio, peak ground acceleration and energy loss during impact on the system responses.

Mouzakis and Papadrakakis [10] have investigated the linear and nonlinear structural response of three-di- mensional adjacent buildings with aligned rigid horizontal diaphragms. The developed formulation takes into account the three-dimensional dynamic contact conditions for velocities and accelerations based on impulse- momentum relationships using the coefficient of restitution and steromechanical approach. Pant and Wijeyewickrema [11] have carried out the study on three-dimensional simulation of seismic pounding between the RC moments resisting frame considering material as well as geometrical nonlinearities.

In the present paper, the formulations of SDOF for one sided and both sided pounding incidences are presented in details. Both elastic and inelastic material behaviors of the SDOF structures have been considered. The equation of motion of SDOF system for both side pounding is being solved using a computer program developed for this purpose in MATLAB [12] . Few sets of solutions of inelastic response obtained from computer program are also compared with SAP 2000NL software [13] results and with referred publication as well.

2. Models for Impact Simulations and Mathematical Formulation of Fixed Base Inelastic SDOF Structure

Structural pounding became catastrophic when building experiences earthquake, there are several uncertainty in its mathematical modeling and characteristics of buildings. But still, the worldwide researchers have studied this problem by large extent in schismatic way; basically researchers have used two methods to model the dynamic impact between the structures, namely contact element method (Force based method or penalty method) and steromechanical method (Based on impulse-momentum principle and coefficient of restitution considering direct central impact of the colliding bodies). Athanassiadou et al. [14] have stated that the steromechanical model used between the adjacent structural units for the prediction of impact forces has not to be recommended because of multiple numbers of impact of closely space stiff system which remains present for a quite long duration. The steromechanical approach uses the instantaneous impact for which the duration of impact should be very small, which is not true in the case of building pounding. Moreover, this approach cannot be implemented in the widely used commercial available software [15] .

Therefore, in the present paper pounding force investigations should be done as per the contact force mechanism by using linear spring model with some stiffness but no damping.

2.1. Linear Spring Model

A linear impact of stiffness (k_{L}) can be used to simulate impact once the gap between adjacent structures closes. The impact force (F_{c}) at time “t” is given by

, (1)

where, d(t) is the interpenetration depth/overlapping distance of the colliding bodies. This approach is relatively straightforward and can be easily implemented in any commercial available software. However, the energy loss during impact is not taken into account. This model is shown in Figure 1 which has been extensively used for impact simulation by Maison and Kasai [8] in their research work.

2.2. Mathematical Formulation of Fixed Base Inelastic SDOF Structure

The theoretical formulation for modeling of three adjacent fixed base SDOF damped inelastic structure is presented here. The middle structure out of these three adjoining structures are undergoes in both side pounding incidences, whereas the other two structures suffers only one side pounding effects. As shown in Figure 2, the adjacent structures are modeled as SDOF systems with lumped masses m_{1}, m_{2} and m_{3} respectively. The structures shown are separated by distances d_{12} between the first and the second structure and d_{23} between the second and the third structure. The stiffnesses of the three structures are k_{1}, k_{2} and k_{3} and linear viscous dashpot constants for the structures are c_{1}, c_{2} and c_{3}, respectively. Impact between the three buildings has been modeled by introducing a spring and a linear viscous dashpot between the colliding structures which corresponds to a specific model explained in Section 2. The stiffness of the spring between the first two structures is s_{12 }and that between the last two structures is s_{23}. The corresponding dashpot constants are c_{12 }and c_{23}. These elements act only when collision occurs.

Figure 1. Contact elements for impact simulation.

Figure 2. Schematic diagram of the three adjacent fixed base SDOF structures.

The incremental governing equations of dynamic contact motion considering one sided pounding due to seismic input at time “t” can be written as:

(2)

where,;;;, are impact force caused by the damper and spring;;;;;;; and .

The solution of the Equation (2) for SDOF system subjected to one side pounding is obtained using average acceleration Newmark-Beta method (implicit method). The incremental quantities in the above equation are the change in the responses from time “t” to “t + Dt”.

Newmark method adopts approximation as following;

(3)

The parameters that define the acceleration changes in the time step (Dt), and also decide the stability and accuracy of Newmark method. When typical values are setting g = 1/2 and 1/6 ≤ β ≤1/4 (in the current study β is considered as 1/4), from all points of view including accuracy, the results are satisfactory.

The equilibrium equation at time t + Dt is express as follows:

(4)

and can be obtained by solving Equation (2). After submitting them into Equation (4) and some algebra, we can obtain

(5)

where,

u_{t}_{+}_{Dt} can be obtain by solving Equation (5), and also can be obtain according expression as follows:

(6)

(7)

where,;;;;;;;.

Impact force also can be obtained as follows:

(8)

Thus, we can get all the desired results, e.g. displacements, velocity, acceleration and impact force.

Wen [16] proposed the equation for modeling non-linear hysteretic force-deformation behavior, in which the force q(t) (as mentioned in Equation (2) is calculated as

(9)

where, k_{0} is the initial stiffness; a is the non-dimensional ratio of post to preyeilding stiffness; Du is the incremental displacement; Q is the yield strength; and DZ is a non-dimensional hysteretic component satisfying the non-linear first order differential equation expressed as

(10)

where, β, t, A and n are the dimensional parameter which control the shape of the hysteretic loop; u_{y} is the yield displacement and is the incremental displacement. The DZ which can be obtained by solving the differential Equation (9) using the fourth order Runge-Kutta method by

(11)

(12)

(13)

(14)

For elasto-plastic force deformation characteristics, the values of Wen’s parameters are taken as β = t = 0.5; A = 1 and n = 15. In this analysis, buildings are modeled as shear buildings and do not include frame action. Any rotation of the buildings is also neglected.

3. Description of Problem

As an example, the study presented in this paper is focused on pounding between three adjacent fixed-base linear elastic and elasto-plastic SDOF structures by using various contact element approach for the impact simulation. The results of MATLAB program obtained through the analysis of SDOF structure are verified using SAP 2000NL software and referred published work. The basic study is done for elastic and inelastic (elasto- plastic) structures with and without pounding by considering linear spring gap element for pounding simulations,

**Structural Properties**

m_{1} = 2500 kg, m_{2} = 4500 kg, m_{3} = 9800 kg, natural frequency of left structure w_{1} = 1 Hz, natural frequency of middle structure w_{2} = 2 Hz, natural frequency of right structure w_{3} = 3 Hz, damping ratio (*ξ*) = 5%, damping constant (c) = 2mw_{n}ξ, yield strength of left structure Q_{1} = 6810 N, yield strength of middle structure Q_{2} = 15,633 N and the yield strength of right structure Q_{3} = 38,301 N.

The properties of linear oscillators were taken from published paper of Mate et al. [17] .

**Gap Element Properties**

The contact element approach has its drawback due to incorrect value of spring stiffness to be used in the numerical studies because of improper correlation of analytical model with the experimentation. Uncertainty in the impact stiffness arises from the unknown geometry of impact surfaces, uncertain material properties under loading and variable impact velocities. The contact spring stiffness is typically taken as the in-plane axial stiffness of the colliding structure. Using a very high stiffness can lead to numerical convergence difficulties and unrealistically high impact forces, whereas taking a very small stiffness can lead to more number of impacts with small impact forces. Therefore, the solution difficulty occurs from the large changes in stiffness upon impact or contact loss, thus resulting in large unbalanced forces affecting the stability of the assembled equation of motion. Here, the value of gap element stiffness is taken as s_{12} = s_{23} = 500,000 N/m for model. Separation distance of all adjoining structures is considered to be constant as d_{12} = d_{23} = 0.025 m. The Impact forces are calculated from the respective pounding force equation of each model.

The characteristics of four real-earthquakes used for the present study are given in Table 1. All the records are taken from the PEER strong motion database (http://peer.berkeley.edu/smcat/). The ground motion records selected for the present work are in moderate range having PGA 0.35 g to 0.5 g (g = acceleration due to gravity 9.81 m/sec^{2}). The output of the time domain analysis is measured in terms of floor displacement and impact forces at the pounding levels for the entire duration of time history at an interval of 0.02 second. The floor acceleration response spectra plots for selected cases are also presented and discussed in the next section.

4. Results and Discussions

Analytical study of the adjacent SDOF structures is carried out using a computer program developed in MATLAB and their results are presented in this section. The basic analytical study is done between elastic and inelastic (elasto-plastic) structures with and without TMD by considering linear spring gap element mechanism for impact simulation for all four ground motion excitations. Prior to carry out the proposed analytical work, some validation study for the developed MATLAB program is also presented here.

4.1. Validation of MATLAB Program Solution with SAP 2000NL Results

Validation of MATLAB program is carried out in two stages, the first stage of validation of MATLAB program is done on SAP 2000NL software results. In the first stage validation stick models are considered as inelastic in nature. While in second stage of validation, the developed MATLAB program results are compared with some standard published paper results.

The first stage of validation as mentioned earlier is done for Model I (linear spring impact simulation model) only of Section 3. For the stick models of three adjacent damped SDOF structure (with or without pounding) of Model I, the structural and gap element properties are taken same as that mentioned in Section 3. It is to be noted here that SAP 2000NL has some limitation such as it can model the adjacent buildings by using the linear spring gap element or by appropriate spring-damper gap element only in which the damping is constant throughout process of time integration. Thus, it is understood that SAP 2000NL can model the structure for linear or Kelvin impact simulation techniques only. However, apart from this limitation, it can very easily reproduce the results for Model I with reasonable degree of accuracy. So, in the present paper the Model I is considered for comparison of results. For this validation following two cases are considered.

Case 1―Model I is analyzed by developing MATLAB program (MATLAB Model)

Case 2―Model I is analyzed on SAP 2000NL software (SAP Model)

Relative study of Model I is developed for fixed-base SDOF structures considering the Northridge ground motion. The results of comparison between SAP model and MATLAB program are presented in Figure 3.

Table 1. Characteristics of real earthquakes used for the present study.

(a)(b)(c)(d)(e)(f)(g)(h)

Figure 3. MATLAB program response validation of inelastic three adjacent structures with SAP software. (a) Displacement time history plot of left building with pounding; (b) Displacement time history plot of left building without pounding; (c) Displacement time history plot of middle building with pounding; (d) Displacement time history plot of middle building without pounding; (e) Displacement time history plot of right building with pounding; (f) Displacement time history plot of right building without pounding; (g) Impact force time history plot between left-middle buildings; (h) Impact force time history plot between middle-right buildings.

From the comparative results, it is noted that the response of Model I obtained from SAP 2000NL and also from MATLAB code are in good agreement. The displacement response of SDOF structures obtained from MATLAB program is much identical to that of the response of SAP 2000NL software. The results of number of collisions and magnitude of impact forces between the adjacent structures in both the cases are reasonably matches to each other. Number of contacts between left and middle structure of SAP model and MATLAB program is 9 and 10 respectively; whereas the number of collisions between middle and right structures obtained from SAP and MATLAB model is 10 and 12 respectively. As per as magnitude of impact forces are concerned, the left-middle structure interaction gives 4.44 kN and 4.08 kN impact forces respectively, while the middle- right structure interaction produces 40 N and 55 N impact forces respectively. But after referring the values of peak impact forces of both the cases, one can easily find slight discrepancies between the values of SAP and MATLAB results that’s because of no control over the software default properties. Thus, from this part of validation work, it is observed that for the preliminary investigation of pounding in inelastic structures, the SAP 2000NL software is much considerable option for the seismic analysis. Moreover, it is also noted that the results of the formulation of MATLAB code are much satisfactorily matches with the result of SAP 2000.

The second stage of validation for the developed code of MATLAB is done for Model IV (Hertz impact simulation model) with the following structural and gap element properties as mentioned by Pantelides and Ma [5] . The Model IV results are evaluated for El Centro ground motion input. The results of MATLAB code are compared with the published paper results of Pantelides and Ma [5] . The results are noted in terms of pounding force time history (refer Figure 4) and displacement time history (see Figure 5) at floor levels of left flexible building. A SDOF structural system is used for one sided pounding, left structure is considered as flexible one and it is collided over the right extremely rigid structure. The inelastic structural systems has been considered by the authors in the published papers, there details are given below.

Structural and gap element details: mass of left flexible structure is 87,550 kg, stiffness of left flexible system is 3500 kN; yielding ductility ratio of inelastic left system is 4; time period of rigid right structure is very small nearly equal to zero; damping ratio of left system is 2% critical; separation distance between adjacent structural units is 0.025 m; and impact stiffness parameter of hertz contact element is 80,000 kNm^{−3/2}.

After the careful assessment of Figure 4 and Figure 5, it is observed that the MATLAB code is much accurate and it could be used reasonably for to predict the pounding response of adjacent structures under any impact simulation techniques. From Figure 4, it is noted that the peak displacement of left SDOF structure in absence and presence of pounding as per the published paper by Pantelides and Ma [5] is around 0.127 m and −0.124 m respectively, while in developed program, these are obtained as 0.135 m and 0.115 m respectively, so displacement response of SDOF structure of MATLAB code are in good agreement with results of Pantelides and Ma [5] . However, some disagreement in displacement results is due to the fact that the time step size considered by Pantelides and Ma [5] is not known. In the present analysis the time step size is taken as 0.02 second. Figure 5 shows that the maximum impact force between two adjoining flexible and rigid SDOF structure at floor level of referred paper is almost 1205 kN (with number of impacts equal to 2), however in MATLAB program this values is obtained as 1103 kN (with number of impacts equal to 3). That means the developed MATLAB code gives consistent pounding forces as that of Pantelides and Ma [5] results. But here, one particular observation is that the numbers of pounding forces obtained by the Pantelides and Ma [5] work are slightly lower than the MATLAB results, that’s again due to the same reason of undefined time step size of time history analysis by the Pantelides and Ma [5] paper.

4.2. Comparative Study of Elastic and Inelastic Three Adjacent SDOF Structures

As mentioned earlier, in this subsection the comparison is being carried out amongst between elastic and inelastic (elasto-plastic) three adjacent SDOF structures considering with and without pounding. For all these comparative work the seismic input is in the form of ground motion excitation, which has given in Table 1. This entire comparative study is being carried out for Model I only (i.e. linear spring used as gap element with some stiffness but no damping) by considering the data of Section 3. The result of comparative study is measured in the form time history plots and tables like displacement time histories for all considered ground motions and are shown in Figures 6-8; impact force time histories are plotted in Figure 9, Figure 10 for all ground motions; the peak displacement values are given in Table 2; and the peak impact forces due to pounding interaction between the structures in all ground excitations are put into a Table 3. For inelastic (elasto-plastic) left, middle and right structures the force deformation plots are also drawn separately as shown in Figures 11-13 respectively. During collision of structures there is sudden break of displacement at the pounding levels results in large and quick short duration acceleration pulses in the opposite direction causes a greater damage to the structures. To study this effect, the spectral acceleration values at floor levels of all three adjoining structures subjected with and without pounding for Superstition Hills ground motion is also plotted in Figure 14. The spectral acceleration values are plotted maximum up to 3 second at an 0.1 second interval by considering either linear elastic behavior or elasto-plastic behavior of structures.

(a)(b)

Figure 4. Displacement time history validation of MATLAB program with the results of Pentelides and Ma [1998]. (a) Results of MATLAB program; (b) Results of published paper of Pentelides and Ma [1998].

(a)(b)

Figure 5. Impact force time history validation of MATLAB program with the results of Pentelides and Ma [1998]. (a) Results of MATLAB program; (b) Results of published paper of Pentelides and Ma [1998].

(a)(b)(c)(d)

Figure 6. Displacement-time history plots of elastic and inelastic left structure (consider gap of 0.025 m and Model I for this study). (a) Response from Northridge ground motion; (b) Response from Cope Mendocino ground motion; (c) Response from Loma Prieta ground motion; (d) Response from Superstition Hill ground motion.

(a)(b)(c)(d)

Figure 7. Displacement-time history plots of elastic and inelastic middle structure (consider gap of 0.025 m and Model I for this study). (a) Response from Northridge ground motion; (b) Response from Cope Mendocino ground motion; (c) Response from Loma Prieta ground motion; (d) Response from Superstition Hill ground motion.

(a)(b)(c)(d)

Figure 8. Displacement-time history plots of elastic and inelastic right structure (consider gap of 0.025 m and Model I for this study). (a) Response from Northridge ground motion; (b) Response from Cope Mendocino ground motion; (c) Response from Loma Prieta ground motion; (d) Response from Superstition Hill ground motion.

(a) (b)(c) (d)

Figure 9. Impact force time history plots due to the pounding interaction between elastic and inelastic left-middle structure (consider gap of 0.025 m and Model I for this study). (a) Response from Northridge ground motion; (b) Response from Cope Mendocino ground motion; (c) Response from Loma Prieta ground motion; (d) Response from Superstition Hill ground motion.

(a) (b)(c) (d)

Figure 10. Impact force time history plots due to the pounding interaction between elastic and inelastic middle-right structure (consider gap of 0.025 m and Model I for this study). (a) Response from Northridge ground motion; (b) Response from Cope Mendocino ground motion; (c) Response from Loma Prieta ground motion; (d) Response from Superstition Hill ground motion.

(a) (b)(c) (d)(e) (f)(g) (h)

Figure 11. Force deformation behavior of inelastic left structures for various ground motions in the absence and presence of pounding (consider gap of 0.025 m and Model I for this study). (a) Response to Northridge with pounding; (b) Response to Northridge without pounding; (c) Response to Cope Mendocino with pounding; (d) Response to Cope Mendocino without pounding; (e) Response to Loma Prieta with pounding; (f) Response to Loma Prieta without pounding; (g) Response to Superstition Hills with pounding; (h) Response to Superstition Hills without pounding.

(a) (b)(c) (d)(e) (f)(g) (h)

Figure 12. Force deformation behavior of inelastic middle structures for various ground motions in the absence and presence of pounding (consider gap of 0.025 m and Model I for this study). (a) Response to Northridge with pounding; (b) Response to Northridge without pounding; (c) Response to Cope Mendocino with pounding; (d) Response to Cope Mendocino without pounding; (e) Response to Loma Prieta with pounding; (f) Response to Loma Prieta without pounding; (g) Response to Superstition Hills with pounding; (h) Response to Superstition Hills without pounding.

(a) (b)(c) (d)(e) (f)(g) (h)

Figure 13. Force deformation behavior of inelastic right structures for various ground motions in the absence and presence of pounding (consider gap of 0.025 m and Model I for this study). (a) Response to Northridge with pounding; (b) Response to Northridge without pounding; (c) Response to Cope Mendocino with pounding; (d) Response to Cope Mendocino without pounding; (e) Response to Loma Prieta with pounding; (f) Response to Loma Prieta without pounding; (g) Response to Superstition Hills with pounding; (h) Response to Superstition Hills without pounding.

(a)(b)(c)

Figure 14. Acceleration response spectra in elastic and inelastic adjacent structural units due to Superstition Hills ground motion inputs (consider gap of 0.025 m and Model I for this study). (a) Left structure; (b) Middle structure; (c) Right structure.

Table 2. Peak displacements of adjoining elastic or inelastic structures for recorded ground motions (considering gap of 0.025 m and Model I for the study).

Note: Negative sign indicate the displacement is along backward direction of applied ground excitation.

Table 3. Absolute impact forces and number of impacts between the adjacent elastic or inelastic structures for recorded ground excitations (considering gap of 0.025 m and Model I for the study).

Note: The values in the brackets indicate the number of collisions between the structures.

From displacement time history plots of Figures 6-8 and Table 2, it is observed that the left structure suffers more displacements than the middle and right structures irrespective of structure is modeled as elastic or inelastic. In middle and right structures, it is noted that the elastic behavior of these structures gives more displacement than the inelastic structural behavior, while in the left structure the inelastic behavior seems to be crucial as per as displacements are concerned. When the comparison is made separately for elastic structure with presence and absence of pounding, it shows that in most of the adjoining structures with the absence of pounding offers more values of displacements. Similarly, when the comparison is done between with and without pounding structures for inelastic case, it shows that in most of the adjoining structures the peak values of displacements are obtained when the pounding is takes place in the structures. One noticeable observation is that in right structures the displacements are same in the absence or presence of pounding. The inelastic left structure with pounding undergoes into more displacements than any other case due to all seismic inputs. While, the right elastic structure with pounding produces more displacements than other three considered cases in all seismic excitations. Due to pounding, the left structure with inelastic behavior is deflected permanently towards the negative direction of applied ground excitations in most of seismic inputs, while these phenomena is much sensitive in other two structural system (i.e. middle or right structure) in inelastic phase.

After studying impact force time history plots from Figure 9, Figure 10 and peak impact forces from Table 3, it is seen that in inelastic structures less amount of impact forces (magnitude-wise and number-wise) are generated during collision of structures. Northridge ground motion produce much catastrophic effect in the structures than any other considered ground motions. In the interaction of left-middle structures, the impact forces are getting higher in magnitude and in numbers than that of the interaction amongst middle-right structures, this proves that the pounding between flexible-rigid structures generates more impact forces than rigid-rigid structures with sufficient separation distance.

After careful study of force-deformation hysteretic of Figures 11-13, it is observed that the left structures undergoes into more plastic stage deformation than any other structures which ultimately lefts some permanent deformation in the structure at the end of the seismic excitation. One more particular observation is that in the right structure, the plastic stage deformation is much lesser than any other structures because of its rigidity. There finds much difference in the force-deformation hysteretic loops of flexible inelastic structures, when pounding is ignored or considered in the structures.

Through figures of floor spectral acceleration plots (Figure 14), it is clearly noticed that left structures attracts more amount of acceleration than the middle and right structures sequentially, which indicate that the flexible structures suffers more damages than that of rigid structures. One important observation in flexible structure is that after attaining the peak acceleration values for a certain period, the further successive values are not lower down drastically, but it remains flatter with a quite high accelerations. In middle and right structures the peak spectral acceleration values are shifted towards the lower time period. In end right structures the peak spectral acceleration values are condensed into a narrow band whereas for other two structures these values are spread up into much wider band. One specific observation in right structure is that their shows much less difference in the values of floor spectral acceleration with the presence and absence of pounding in elastic or inelastic behavior of structures. Pounding always produces more amount of acceleration in the structures than without pounding structures irrelevant of elastic or inelastic behavior. Elastic structure always overestimates the floor spectral acceleration than inelastic structure in case of pounding, that’s because of more number of impact takes place in elastic structure, on the other hand, the inelastic structure always have a chance to change the axis of deformation which ultimately results into less numbers of contact with the adjacent structural units.

5. Conclusions

The comparison between the earthquake-induced pounding involved behavior of three adjacent SDOF structures modeled as elastic or inelastic system has been investigated in this paper. The results of the developed MATLAB codes are verified with SAP 2000NL software results as well as with referred published paper results. Four different ground motion records with different PGA have been applied to conduct the numerical simulations. The following specific conclusions, which are subject to limitations of models used, may be drawn from the present study:

1) The results of the study indicate that the responses of elastic system are much different when comparing to the response of inelastic system, specifically, in lighter/flexible building which easily undergoes into yielding stage during pounding. One important observation is that the values of maximum impact forces and the number of impacts are larger in the elastic case than those in the inelastic case.

2) With the presence of pounding, the flexible inelastic structure always has more chances to deform permanently towards the opposite face of pounding, mostly in high and moderate ground excitations. The force-de- formation hysteretic of flexible structure is much sensitive when subjected to pounding. Also, the force-defor- mation hysteretic loop of flexible structure shows much variation when compared in elastic and inelastic systems.

3) The presence of impact forces during pounding in the closely spaced structures significantly increases the spectral acceleration of the structural system. In addition to that during one sided pounding, mostly in flexible structures the peak spectral floor accelerations are normally shifted towards the lower time period of the system. Elastic structure shows much higher floor spectral acceleration values than inelastic structures since more quick acceleration pulses are generated due to more impact forces.

Conflicts of Interest

The authors declare no conflicts of interest.

Cite this paper

*Open Journal of Civil Engineering*,

**6**, 50-73. doi: 10.4236/ojce.2016.61006.

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