Research Article  Open Access
HongYu Jia, XianLin Lan, Nan Luo, Jian Yang, ShiXiong Zheng, Chao Zhang, "Nonlinear Pounding Analysis of Multispan and Simply Supported Beam Bridges Subjected to Strong Ground Motions", Shock and Vibration, vol. 2019, Article ID 8759428, 11 pages, 2019. https://doi.org/10.1155/2019/8759428
Nonlinear Pounding Analysis of Multispan and Simply Supported Beam Bridges Subjected to Strong Ground Motions
Abstract
To investigate the nonlinear impact effect of multispan simply supported beam bridges under strong earthquakes, firstly, the dynamic motion equation, the algorithm of its solution, and some pounding modelling methods are presented and the finite element model of a considered multispan simply supported railway beam bridge is established in the nonlinear finite element software of SAP2000 in which the primary nonlinear characteristics of the bearing and the impact element are considered herein. Secondly, the natural vibration characteristic of the considered railway bridge is analyzed to prepare for the subsequent parameter analysis. Finally, the influence of three nonlinear parameters, i.e., stiffness of impact element, separation gap width of expansion joint, and bearing stiffness, on impact responses of bridge structures is studied. The results show that the first several modes of multispan simply supported beam bridges are mainly longitudinal and vertical vibrations. Under longitudinal seismic excitations, the large longitudinal displacement response is induced possibly and results in the collision or even unseating of superstructures at the expansion joints and abutments. The influence of separation gap width between adjacent decks on the pounding effect of bridges is greater than that of collision stiffness originated from the pounding modelling element. The impact force and pounding number run up to the maximum conditional on the collision stiffness of 9.9 × 10^{9} (N/m) and the separation gap width of 0.14 (m). The bearing stiffness affects significantly the displacement of the pier top and the crosssectional internal force at the bottom of piers but has little effect on the collision force and number.
1. Introduction
Multispan simply supported beam bridge type is widely used in railway bridges on account of the advantages such as fast construction, standardized and assembled components, and convenient manufacture and installation. Moreover, the multiple span bridges are often built with the expansion joints to accommodate temperature and numberdependent deformations. However, the expansion joints between two adjacent decks or between deck and abutment will be vulnerable components under strong ground motions, thanks to the superstructure pounding which may excite the local failure of deck itself and even catastrophic unseating damage.
Recently many earthquakes, e.g., Wenchuan earthquake (2008, M8.0) [1], Chile earthquake (2010, M8.8) [2], North Sumatra earthquake (2012, M8.5), and Nepal earthquake (2015, M8.1) in the world occurred frequently whose magnitudes increased intensely as well. Meanwhile, these ground motions caused casualties, economic losses, and collision and collapse of structures including buildings and bridges. Hence, an increasing number of scholars all over the world have paid great attention to the collisions especially for the bridge pounding occurred between adjacent decks and between deck and abutment. Because of the complexity of the collision mechanism, it is extremely difficult to find an accurate fully collision simulation method. However, some practical and handy approaches are developed in recent studies [3–6]. For example, rooted in the law of conservation of energy and momentum, the collision process of building and bridge in earthquakes were simulated by using the method of restoring coefficient [7–10]. Among these scholars, Malhotra indicated the relationship among the restoring coefficient, the material damping ratio of the main girder, and the length ratio of the adjacent girders and considered that the duration of the collision is close to the basic period of axial vibration of relatively short segment in all of girders. The linear spring element was utilized to simulate the seismic impact of expansion joints of bridge structures [11]. The further improved element with the combination of spring and damper was used widely to consider the energy dissipation in the collision process. In general finite element software, e.g., Ansys, Abaqus, and Sap2000, this improved element was named as linear springdamper element [12, 13]. For considering the nonlinear behavior in the pounding process, the nonlinear spring element was employed to model the nonlinear relationship between deformation and stress [14, 15]. As known, the Hertzdamp model based on the nonlinear spring and damper element was developed to consider the energy dissipation, thanks to pounding better [16]. The threedimensional contactfriction model was adjusted to investigate the collision effect between adjacent bridge segments on the responses of bridge structures subjected to ground motions. However, due to the complexity of the contact algorithm this method failed widely to be applied in practical engineering for the investigation of pounding occurred between two adjacent bridge segments [17].
Not only are the methods of collision simulation studied but also the effects of the earthquakeinduced pounding upon the entire and local responses of bridge structures. The isolation parameter analysis of a multispan simply supported beam bridge under spatial varying ground motions was conducted by Zanardo et al. [18] to explore the influence of seismic spatial variability on the impact of bridge segments, and the importance of isolation device installed between deck and pier was illustrated for reducing the bridge damages as a result of the earthquakeinduced pounding. Based on random vibration theory, Hao [19] studied the influence of the damping, geological condition, and magnitude on the width demand of separation gap between two adjacent decks for pounding analysis of simply supported beam bridge under spatial ground motions. And it is expected that nonuniform vibration characteristics of two adjacent bridge segments are the predominant factors owing to asynchronous displacement responses excited by the spatially varying ground motions. On account of the simplified bilinear model, Ruangrassamee and Kawashima [20] proposed the relative displacement spectrum under collision conditions and believed that the pounding can result in the increase of demand width of expansion joints among adjacent segments. Jankowski et al. [21] and Ankowski et al. [22] presented the collision effect of singlecolumn pier viaducts under ground motion excitations on the dynamical responses of structures and many mitigation measures are also introduced to reduce the damages induced by the pounding. Bi et al. [23] assessed the influence of spatial seismic nature, site condition, and pilesoil interaction on the demand of the designed separation gap length in the seismic analysis of bridge structures. Zhang et al. [24] and Jia et al. [25] proposed an efficient, accurate, and probabilistic analysis method for prediction and assessment of impact effects of high pier railway bridges subjected to threedimensional nonstationary multisupport excitations. Won et al. [27] carried out the impact response analysis of multispan simply supported beam bridges under multisupport seismic excitations, but some detailed parameter analysis is insufficient such as stiffness and clearance of impact element. Liolios et al. [28] studied the impact effect of concrete beam bridges with the cablelimit devices fixed between two adjacent decks and expected that the impact was responsible for the bearing and unseating damages. Maragakis et al. [29] performed an elasticplastic dynamical analysis of simply supported beam bridges for taking into account the impact effect between abutment and main girder. Moreover, the nonlinearity of the filled soil behind the considered abutments is considered for studying its influence on the responses of structures. Jankowski et al. [30] analyzed the collision effect occurred at expansion joints of multispan continuous girder bridges on the separation gap size to avoid the pounding.
Following the aforementioned reviews, the nonlinear pounding analysis of multispan simply supported beam railway bridges subjected to strong ground motions is studied rarely. In this study, the threedimensional finite element model of a realistic multispan simply supported beam railway bridge is established based on SAP2000 platform. And the nonlinear properties of bearing and impact element are considered in the dynamical analysis of railway bridge structures. These considered nonlinearities include the width of expansion joint, impact stiffness, and longitudinal stiffness of bearing in the seismic analysis of employed realistic multispan simply supported beam railway bridges for providing indepth insight into predicting or avoiding the collision damages of railway bridge structures.
2. General Theory
2.1. Dynamical Response Equation of Bridge Structures
The equation of motion of the lumped mass system subjected to ground motions can be formulated by expressing the equilibrium of the effective forces associated with each of its degrees of freedom. The force equilibrium of a multidegreeoffreedom lumped mass system as a function of number can be expressed by the following relationship:where represents the inertial force vector acting on the node masses; is a vector of viscous damping, or energy dissipation, forces; denotes a vector of internal forces carried by the structure; and indicates a vector of externally applied forces.
For many structural systems, the approximation of linear structural behavior is made to convert the physical equilibrium statement to the following set of secondorder, linear, differential equations aswhere , , and represent the mass matrix, damping matrix, and stiffness matrix of structures, respectively. , , and represent the absolute acceleration, absolute velocity, and absolute displacement of the structural system, respectively.
2.2. Hilber–Hughes–Taylor α Algorithm
Heretofore, the motion equation of the lumped mass system subjected to ground motions can be solved by several available methods, e.g., Newmark method, Wilson method, permutation method, Hilber–Hughes–Taylor (HHT) method, and Chung–Hulbert method. These methods have the same characteristics of implicit integration and unconditional stability. The Newmark method is the earliest method for dynamic solution, and some latter methods are modified or improved based on the Newmark method. It assumes the acceleration between arbitrary number intervals varies linearly in the dynamic analysis of structures. Thus, the iterative calculation is essential to the Newmark method which results in a significant amount of number to solve structural systems with just a few hundred degrees of freedom as a result of the large computational requirements.
In order to solve the above equations of motion, the improved Newmark method is used. This theory is briefly introduced below. Consider the solution of the linear dynamic equilibrium equations for one degree of freedom written in the following form [31]:
The direct use of Taylor’s series provides a rigorous approach to obtain the following two additional equations:
Newmark truncated those equations and expressed them in the following form:
If the acceleration is assumed to be linear within the time step, the following equation can be written:
The substitution of equation (7) into equations (5) and (6) produces Newmark’s equations in standard form:
The Newmark method is the earliest method for dynamic solution and some latter methods are modified or improved based on the Newmark method. It assumes the acceleration between arbitrary time intervals varies linearly in the dynamic analysis of structures. Thus, the iterative calculation is essential to the Newmark method which results in a significant amount of time to solve structural systems with just a few hundred degrees of freedom as a result of the large computational requirements.
For improving the computational efficiency and removing the numerical damping in highorder modes in structural analysis, Wilson introduces a coefficient θ to eliminate the fluctuation around real solution because of no unconditional stability in the Newmark method. Furthermore, HHT method is developed by introducing another coefficient α to modify the structural dynamic equation on the basis of the Newmark method. The modified dynamic equation is written as [31]where, , and are the acceleration, velocity, and displacement at time “,” respectively; and are the velocity and displacement at time “,” respectively; and is limited in the range of [0, 1/3]. The method is equivalent to the average acceleration method when in HHT. Thus, the HHT method is also called modified average acceleration method and is the most accurate in all of numerical methods. Nevertheless, the negative value of is usually adopted to dissipate the highfrequency energy and better convergence.
3. Pounding Theory
Usually the bridge superstructure pounding occurs due to their outofphase movements once the relative displacement response of adjacent segments exceeds the separate distance (gap). As known, it is fairly difficult to model the pounding process based on the general finite element software platform due to its geometric and material complexity. Moreover, impact forces are applied and removed during a desperately short number, and the process of energy transfer is highly complicated [32]. Even though a precise simulation of pounding is difficult, various researches have been analytically studied based on two techniques. One is a stereo mechanical approach and the other is forcebased approach. The stereo mechanical approach uses the principle of momentum conservation and the coefficient of restitution to modify the velocities of colliding structures after impact. The forcebased approach utilizes contact elements consisting of a spring and a damper, which are extensively studied by many researchers. In brief, two main methods, the restoring coefficient method and the contact element method, for simulating the impact of bridge structures under earthquakes are presented herein.
3.1. Restoring Coefficient Method
Based on the assumption that the pounding is an impact occurred between two particle centers and is completed instantaneously, and the elasticplastic impact is modelled by the restoring coefficient for the determination of velocity after pounding. In dynamical analysis of pounding according to the law of conservation of energy and momentum, the velocity of two particles after pounding can be obtained aswhere and denote the separate velocity of two particles after pounding, respectively; and represent the velocity of two particles before collision; and represent the mass of two pounding particles, respectively; and e is the restoring coefficient and decided by the following expression:
The different values of recovery coefficient represent different collision states; i.e., e = 0 represents the complete elastic collision. Besides, Anagnostopoulos and Spiliopoulos [33] studied the collision problem of related structures under earthquakes by using the method of restoring coefficient and considered that the range of restoring coefficient is generally between 0.5 and 0.75 for solid collision of structures. Azevedo and Bento [34] suggested that the e value of typical concrete structures should be 0.65 on the basis of relevant experimental results. The main girder collision of viaducts is investigated theoretically and experimentally, and an important conclusion is drawn that the value of e should be reduced appropriately for the plasticity. Overall, the restoring coefficient method owns much many virtues, e.g., clear physical concept, simple algorithm, and understanding readily though it is based on the simplified impact model of two particles. But it cannot take into account the collision compression deformation of the contact areas and neglects the instantaneous stress and deformation in the collision phase. For bridge structures with larger mass and smaller elastic modulus, the impact deformation is larger and the duration is longer relative to other structures. It will be unreasonable to ignore the instantaneous stress and deformation in the impact stage. In addition, the restoring coefficient method is a dynamic collision simulation method and not yet forcebased method.
3.2. Contact Element Method
Nowadays for the impact simulation of structures, the contact element method is an exceedingly fashionable algorithm embedded in general or professional finite element software such as Ansys, Abaqus, Sap2000, and Opensees. As regard to the contact element method, it is activated when superstructures of bridges are in contact and impact. Commonly, the contact element is composed of a spring with high stiffness to avoid material overlap and ensure short collision duration and a damper connected in parallel with the foregoing spring to simulate energy dissipation during collision. Generally contact elements include linear spring element, linear springdamper element, nonlinear spring element, nonlinear springdamper element, improved nonlinear springdamper element, and threedimensional contactfriction element [35]. The linear spring element is the simplest in all, but it cannot consider the energy dissipation in the collision process so that the simulation accuracy and effect is also the worst. Threedimensional contactfriction element can effectively simulate arbitrary collision between adjacent bridge segments and can also be implemented in numerical integration methods. However, it takes a lot of computing number to find contact pairs. Meanwhile, the calculation algorithm is quite complicated which restricts the development and application of this method to a certain extent.
In this study, the nonlinear gapcrush element from SAP2000 is utilized to simulate the impact of bridge superstructures [36]. This gapcrush element has following physical properties:(1)Until the opening gap is closed, the used element cannot develop a force. A negative value of signifies an initial compression force.(2)The element can only develop a negative compression force. The first yield deformation is specified by a positive number.(3)The crush deformation is always a monotonically decreasing negative number.
The gap part of gapcrush element is set to study the collision among the adjacent decks of multispan simply supported beam bridges under earthquakes. The entire model is composed of a spring and an open gap in series. Its behavior is described as follows:where is the iterative force, is the yield stiffness, is the initial linear stiffness, is the elastic deformation， is the compression deformation at number t, is the crush deformation at the end of collision, and is the initial value for expansion joint.
4. Bridge Model and Dynamic Characteristic Analysis
4.1. Finite Element Model
For providing an indepth insight into the pounding effect of multispan simply supported beam railway bridges under strong earthquakes a precast ballastless track posttensioned prestressed concrete simply supported box girder (double track) railway bridge is employed in this study. As shown in Figure 1, this used railway bridge has span distribution of 6 × 31.5 (m) and the width 12.6 (m) of the bridge deck. The box section is adopted in the main girder with variable section at the end support. In addition, the cross section of the rectangular solid pier is variable in the range of 3 meters below the bottom of the main beam and is equal in the range of 3 meters. The height of each pier is 14 meters.
Each single span girder is supported by four basin rubber bearings, i.e., lateral movable bearing, longitudinal movable bearing, multidirectional movable bearing, and fixed bearing. The support arrangement of this railway bridge is shown in Figure 1. Moreover, the threedimensional dynamic nonlinear analysis model of the multispan simply supported beam bridge is established by using the finite element software SAP2000, as shown in Figure 2. Both pier and girder are modelled by frame beam element, while the basin rubber bearings are modelled by using Wen plastic elements with nonlinear property. The restoring force model is given as follows:where is the longitudinal stiffness of bearing, is the yield force, indicates the specified ratio of postyield stiffness to elastic stiffness, z is the internal lag variable, and its restoring force model is also shown in Figure 2.
4.2. Dynamic Characteristic Analysis
Because the longitudinal dimension of the bridge is excessively larger than transverse one, the pounding of decks and even pulloffanddrop collapse are more likely to occur under the longitudinal seismic excitation. Therefore, this paper mainly studies the superstructure collision of bridges under the longitudinal seismic excitation. The natural vibration characteristics of bridges are the basis of dynamic analysis and has important role on the responses of structures. Due to the limited space, only the first six natural frequencies and modes are listed in Table 1. As seen in Table 1, the longitudinal vibration of both first two modes implies the potential pounding possibilities occurred in the longitudinal of the bridge.

5. Numerical Analysis and Case
5.1. Case
In order to study the nonlinear impact effect of multispan simply supported beam bridges under strong earthquakes, the artificial ground motion [37] is used as the excitation source in the nonlinear dynamic analysis. The open and impact stiffness values of gap/crush element are determined by a series of discrete values, namely, the open values are used, e.g., 0.1 m, 0.12 m, 0.14 m, 0.16 m, and 0.18 m, and the impact stiffness, i.e., 9.8 × 10^{9} (N/m), 9.9 × 10^{9} (N/m), and 1.0 × 10^{10} (N/m), is ascertained in near the range of main girder stiffness [38]. Hence, totally 15 calculation cases are obtained according to the combination of and impact stiffness.
5.2. Parameter Analysis
5.2.1. Force and Number of Collision
The pounding effect problem of bridges can be reflected by the collision contact force and number of pounding of bridges subjected to strong ground motions. For better pertinence, only the impact force and number of collision on the top of pier 1# will be discussed in detail. The relationship between the impact force and number of collision and the impact stiffness and value is shown in Figures 3 and 4, respectively.
As seen in Figures 3 and 4, the overall trend of collision force varied consistently with different impact stiffness. The impact force increases firstly and then decreases drastically. The maximum collision force (about 9.62 × 10^{7} (N)) occurs at the value of 0.14 m and the collision stiffness of 9.9 × 10^{9} (N/m). This performed analysis herein can derive the maximum impact force which may cause a serious damage to bridge structures under seismic excitations and provide a most critical design control point for engineers. From Figure 4, it reveals that the number of collision decreases with the increase of value because adequate separation length between adjacent two decks can accommodate the relative displacement responses. When the value changes from 0.10 m to 0.14 m, the number of collisions decreases slowly. When the value is greater than 0.14 m, the number of collisions decreases significantly. It shows that the value of 0.14 m is the change point. At the value of 0.14 m, the collision number at the impact stiffness of 9.9 × 10^{9} (N/m) is 50. Therefore, when the impact stiffness of the collision element is 9.9 × 10^{9} (N/m) and the value is 0.14 m, it is the most disadvantageous condition. It should be noted that the reasonable separation gap width needs to ensure a smooth traffic flow. Namely, it is not that the longer the separation gap length is, the better the mitigating impact effect is.
The time history of impact force in Figure 5 shows the pounding occurs mainly at three number intervals, i.e., 15–20 (s), 30–32 (s), and 37–41 (s). During each pounding number interval, the pounding force increases firstly and then reduces to zero lasting to the beginning of next collision. From Figure 6, it can be revealed that the pounding occurs once the longitudinal relative displacement response exceeds the value of 0.14 m confirmed in impact element. Additionally, the impact number observed from longitudinal relative displacement response in Figure 6 is consistent completely with that obtained from impact force aspect in Figure 5.
5.2.2. Displacement Response
The impact parameters (stiffness and open value) are discussed only from the view point of impact element. The validity of the above conclusions is further verified from the angle of pier top displacement. The peak displacement on the top of pier 1# is shown in Table 2. In the column of working conditions in Table 2, 0.1 of “0.1–9.8” represents the value of 0.1 m, while 9.8 represents the impact stiffness of 9.8 × 10^{9} (N/m) and so on.

From the overall analysis in Table 2, it can be seen that the displacement of pier top decreases with the increase of impact stiffness and value. Under the same value and different stiffness values, the peak displacement of the pier top of the same pier is approximately close. This indicates that the impact stiffness has little effect on the displacement responses. While under the same impact stiffness with different values, the peak displacement of the pier top of the same pier varies greatly, which indicates that the pier top displacement is more sensitive to the value. When the value is greater than 0.14 m, the peak displacement of almost every pier top is relatively stable. That is to say, the peak displacement of pier top turns at the value of 0.14 m, and no longer drops. This is consistent with the results of the analysis of collision force and number of collisions mentioned above. Therefore, the collision parameters of the collision element are taken as the most disadvantageous values, i.e., the stiffness is 9.9 × 10^{9} (N/m) and the value is 0.14 (m).
Figure 7 is the displacementime history of the pier top under the most disadvantageous conditions. The analysis shows that the displacement of the pier top changes in the same law, first increases, then decreases, and finally increases. Finally, the reason for the increase is the lag of response caused by inertia, which is the same as the collision force time history mentioned above. Figure 8 shows the longitudinal displacement of the deck, which the change trend is consistent with Figure 7, which shows that the main girder and piers are well connected, and they can well deform together. Under the action of earthquake, the support has not been damaged.
5.3. Analysis of Bearing Parameter
Many bearings are usually used in multispan simply supported beam bridges, and different bearing parameters will seriously affect the collision of bridge structures under earthquakes. Therefore, it is very important to explore the influence of bearing parameters on collision. The optimal collision parameters of the collision element have been determined in Section 2.2 above. In this section, the gap element with the optimal parameters is used to analyze the different bearing stiffness and explore the influence of the support stiffness on the responses of structures. According to Table 1, the first six modes of vibration are mainly longitudinal and vertical vibration, so the effect of the bearing longitudinal stiffness on the impact results is discussed hereon in this study. The bearing stiffness is discretized into points, e.g., 0.8 × 10^{6} N/m, 0.9 × 10^{6} N/m, 1.0 × 10^{6} N/m, 1.1 × 10^{6} (N/m), 1.1 × 10^{6} (N/m), 1.2 × 10^{6} (N/m), 1.3 × 10^{6} (N/m), 1.4 × 10^{6} (N/m), and 1.5 × 10^{6} (N/m), for investigating the influence of bearing stiffness on the collision. The results of this study are also are discussed from the views of collision force and number.
5.3.1. Collision Force and Number
The peak value of collision force and the numbers under the condition of different longitudinal bearing stiffness are shown in Table 3.

As observed from Table 3, the peak impact force and number of collision experience grow initially, then descend, and eventually ascend with the increase of the longitudinal stiffness of the bearing. For simulating the most disadvantageous situation, further the longitudinal stiffness of the bearing is locked at the value of 1.0 × 10^{6} (N/m), because the collision force and the number are the maximum in entire analysis process.
5.3.2. Displacement Response on the Top of Pier 1# and Deck
The top displacement of pier 1# and longitudinal displacement of the deck can reflect the degree of collision of simply supported beam bridges from another angle. The varying tendency of displacement response can be observed readily in Table 4 and Figures 7 and 8 with different longitudinal stiffness of bearing.

Generally speaking in Table 4, the peak displacement of each pier decreases with the increase of bearing stiffness. This variation depends primarily on two reasons that one is larger stiffness resisting displacement and the other is that the factor is the energy dissipation function of rubber bearing. The bearing is the most vulnerable component in all bridge components under earthquakes. The greater the longitudinal stiffness of bearing, the more restrictive the longitudinal deformation of piers and girders under earthquakes. The range of longitudinal displacement of deck varies from 0.4090 m to 0.4588 (m). The longitudinal displacement of the main girder decreases with the increase of the stiffness of bearing, but there is a sudden change when the stiffness is 1.0 × 10^{6} (N/m) and the maximum value is 0.4588 (m). It can be concluded that collision is more likely to occur when the stiffness of the support is 1.0 × 10^{6} (N/m).
In addition, Table 4 is represented from the aspect of graphic for providing more clearly the changing trend. As seen in Figure 9, the top displacements of 2# pier and 4# pier, and 1# pier and 5# pier are relatively close, respectively, yet the top displacement of 3# pier is the smallest, thanks to the structural arrangement symmetrically. Therefore, based on the symmetry of bridge structure, the longitudinal stiffness of the bearing on the side pier may relatively be large in practical engineering. Consequently one can observe more intuitively from Figure 9 that the longitudinal displacement of the main girder has changed abruptly when the stiffness of the bearing is 1.0 × 10^{6} (N/m).
5.3.3. Internal Force at the Bottom of Pier
A simply supported beam bridge not only suffers from the damage of main beams but also suffers from the shear failure, bending failure, and bendingshear failure of pier bottom. In order to avoid this kind of damage, it is fairly necessary to check whether the bearing capacity of pier bottom section meets the requirements.
The shearing force and moment at the bottom of piers is listed in Tables 5 and 6, respectively, with different support stiffness. The shearing force and moment decrease implicitly with the increase of the longitudinal stiffness of the bearing. The maximum shearing force at the bottom of piers is 7.935 × 10^{7} (N) occurred at the bottom of piers 1# and 2# and the stiffness of the bearing is 1.0 × 10^{6} (N/m). The moment at the bottom of each pier is also the largest at the stiffness of 1.0 × 10^{6} (N/m). It shows that when the stiffness of the bearing is 1.0 × 10^{6} (N/m), the internal force at the pier bottom reaches a larger value which considered as the most disadvantageous situation.


6. Conclusion
In this study, the nonlinear pounding analysis of a multispan simply supported beam bridge is performed and the following conclusions are drawn:(1)A threedimensional finite element model of a multispan simply supported beam bridge is established based on the finite element software of SAP2000. The first two modes of vibration of the considered multispan simply supported beam bridge are mainly longitudinal vibration which may result in the longitudinal pounding.(2)The selection of collision parameters, e.g., the bearing stiffness, the width of expansion joint, and the impact element stiffness, greatly affect the responses of the multispan simply supported beam bridge subjected to ground motions. The stiffness of 9.9 × 10^{9} (N/m) and the value of 0.14 (m) in the impact element can cause most unfavorable responses of structures.(3)Although the longitudinal stiffness of the bearing has little effect on the impact force and number, it will affect the displacement at the top of piers and the internal force at the bottom of piers to a large extent.
Data Availability
All the data used to support the findings of this study are included in the paper.
Conflicts of Interest
The authors declare that they have no conflicts of interest.
Acknowledgments
The research for this paper was supported by the Science and Technology Plan of Sichuan Science and Technology Department (No. 2019YJ0243), National Science Foundation of China (No. 51308465), and Postdoctoral Science Foundation of China (No. 2015M580031). The authors would like to express their sincere gratitude to all the sponsors for the financial support.
References
 C. J. Lin, H. Hung, Y. Liu, and J. Chai, “Reconnaissance report of 0512 China Wenchuan earthquake on bridges,” in Proceedings of the 14th World Conference on Earthquake Engineering, Beijing, China, October 2008. View at: Google Scholar
 K. Kawashima, S. Unjoh, J.I. Hoshikuma, and K. Kosa, “Damage of bridges due to the 2010 Maule, Chile, earthquake,” Journal of Earthquake Engineering, vol. 15, no. 7, pp. 1036–1068, 2011. View at: Publisher Site  Google Scholar
 H.Y. Jia, X.L. Lan, S.X. Zheng, L.P. Li, and C.Q. Liu, “Assessment on required separation length between adjacent bridge segments to avoid pounding,” Soil Dynamics and Earthquake Engineering, vol. 120, pp. 398–407, 2019. View at: Publisher Site  Google Scholar
 Q. L. Cheng, Y. Wei, X. Y. Zheng, L. Zheng, and L. Nan, “Base pounding model and response analysis of baseisolated structures under earthquake excitation,” Applied Sciences, vol. 7, no. 12, p. 1238, 2017. View at: Publisher Site  Google Scholar
 H. Naderpour, R. C. Barros, S. M. Khatami, and R. Jankowski, “Numerical study on pounding between two adjacent buildings under earthquake excitation,” Shock and Vibration, vol. 2016, Article ID 1504783, 9 pages, 2016. View at: Publisher Site  Google Scholar
 R. Moghabeli, H. Parastesh, H. Lotfollahian, and M. Parvaresh, “Seismic pounding between adjacent concrete frames,” Seismostruct Letters, vol. 1, no. 2, pp. 1–8, 2018. View at: Google Scholar
 M. J. N. Priestley, F. Seible, and G. M. Galvi, Seismic Design and Retrofit of Bridges, John Wiley and Sons Inc., Hoboken, NJ, USA, 1996.
 C. J. Athanassiadou, G. G. Penelis, and A. J. Kappos, “Seismic response of adjacent buildings with similar or different dynamic characteristics,” Earthquake Spectra, vol. 10, no. 2, pp. 293–317, 1994. View at: Publisher Site  Google Scholar
 R. DesRoches and G. L. Fenves, “New design and analysis procedures for intermediate hinges in multiple frame bridges,” Earthquake Engineering Research Center, University of California, Berkeley, CA, USA, 1997, Report No. UCB/EERC97/12. View at: Google Scholar
 P. K. Malhotra, “Dynamics of seismic pounding at expansion joints of concrete bridges,” Journal of Engineering Mechanics, vol. 124, no. 7, pp. 794–802, 1998. View at: Publisher Site  Google Scholar
 R. Jankowski, K. Wilde, and Y. Fujino, “Reduction of pounding effects in elevated bridges during earthquakes,” Earthquake Engineering & Structural Dynamics, vol. 29, no. 2, pp. 195–212, 2000. View at: Publisher Site  Google Scholar
 S.H. Kim and M. Shinozuka, “Effects of seismically induced pounding at expansion joints of concrete bridges,” Journal of Engineering Mechanics, vol. 129, no. 11, pp. 1225–1234, 2003. View at: Publisher Site  Google Scholar
 S. A. Anagnostopoulos, “Pounding of buildings in series during earthquakes,” Earthquake Engineering & Structural Dynamics, vol. 16, no. 3, pp. 443–456, 1988. View at: Publisher Site  Google Scholar
 H. Y. Gou, W. Zhou, G. D. Chen, Y. Bao, and Q. H. Pu, “Insitu test and dynamic analysis of a doubledeck tiedarch bridge,” Steel and Composite Structures, vol. 27, no. 1, pp. 161–175, 2018. View at: Google Scholar
 K. T. Chau, X. X. Wei, X. Guo, and C. Y. Shen, “Experimental and theoretical simulations of seismic poundings between two adjacent structures,” Earthquake Engineering & Structural Dynamics, vol. 32, no. 4, pp. 537–554, 2003. View at: Publisher Site  Google Scholar
 S. Muthukumar and R. DesRoches, “A Hertz contact model with nonlinear damping for pounding simulation,” Earthquake Engineering & Structural Dynamics, vol. 35, no. 7, pp. 811–828, 2006. View at: Publisher Site  Google Scholar
 P. Zhu, M. Abe, and Y. Fujino, “Modelling threedimensional nonlinear seismic performance of elevated bridges with emphasis on pounding of girders,” Earthquake Engineering & Structural Dynamics, vol. 31, no. 11, pp. 1891–1913, 2002. View at: Publisher Site  Google Scholar
 G. Zanardo, H. Hao, and C. Modena, “Seismic response of multispan simply supported bridges to a spatially varying earthquake ground motion,” Earthquake Engineering & Structural Dynamics, vol. 31, no. 6, pp. 1325–1345, 2002. View at: Publisher Site  Google Scholar
 H. Hao, “A parametric study of the required seating length for bridge decks during earthquake,” Earthquake Engineering & Structural Dynamics, vol. 27, no. 1, pp. 91–103, 1998. View at: Publisher Site  Google Scholar
 A. Ruangrassamee and K. Kawashima, “Relative displacement response spectra with pounding effect,” Earthquake Engineering & Structural Dynamics, vol. 30, no. 10, pp. 1511–1538, 2001. View at: Publisher Site  Google Scholar
 R. Jankowski, K. Wilde, and Y. Fujino, “Pounding of superstructure segments in isolated elevated bridge during earthquakes,” Earthquake Engineering & Structural Dynamics, vol. 27, no. 5, pp. 487–502, 1998. View at: Publisher Site  Google Scholar
 R. Ankowski, K. Wilde, and Y. Fujino, “Reduction of pounding effects in elevated bridges during earthquakes,” Earthquake Engineering & Structural Dynamics, vol. 29, no. 2, pp. 195–212, 2000. View at: Publisher Site  Google Scholar
 K. Bi, H. Hao, and N. Chouw, “Influence of ground motion spatial variation, site condition and SSI on the required separation distances of bridge structures to avoid seismic pounding,” Earthquake Engineering & Structural Dynamics, vol. 40, no. 9, pp. 1027–1043, 2011. View at: Publisher Site  Google Scholar
 D.Y. Zhang, H.Y. Jia, S.X. Zheng, W.C. Xie, and M. D. Pandey, “A highly efficient and accurate stochastic seismic analysis approach for structures under tridirectional nonstationary multiple excitations,” Computers & Structures, vol. 145, pp. 23–35, 2014. View at: Publisher Site  Google Scholar
 H.Y. Jia, D.Y. Zhang, S.X. Zheng, W.C. Xie, and M. D. Pandey, “Local site effects on a highpier railway bridge under tridirectional spatial excitations: nonstationary stochastic analysis: nonstationary stochastic analysis,” Soil Dynamics and Earthquake Engineering, vol. 52, pp. 55–69, 2013. View at: Publisher Site  Google Scholar
 H. Y. Jia, J. G. Zhao, X. Li, L. P. Li, and S. X. Zheng, “Probabilistic pounding analysis of highpier continuous rigid frame bridge with actual site condition,” Earthquakes and Structures,, vol. 15, no. 2, pp. 193–202, 2018. View at: Google Scholar
 J.H. Won, H.S. Mha II, and S.H. Kim, “Effects of the earthquakeinduced pounding upon pier motions in the multispan simply supported steel girder bridge,” Engineering Structures, vol. 93, pp. 1–12, 2015. View at: Publisher Site  Google Scholar
 A. Liolios, A. Liolios, G. Hatzigeorgiou, and S. Radev, “Pounding effects on the earthquake response of adjacent reinforced concrete structures strengthened by cable elements,” Journal of Theoretical and Applied Mechanics, vol. 44, no. 2, pp. 41–56, 2014. View at: Publisher Site  Google Scholar
 E. Maragakis, B. Douglas, and S. Vrontinos, “Classical formulation of the impact between bridge deck and abutments during strong earthquake,” in Proceedings of the 6th Canadian Conference on Earthquake Engineering, pp. 205–212, University of Toronto Press, Toronto, Canada, June 1991. View at: Google Scholar
 R. Jankowski, “Nonlinear viscoelastic modelling of earthquakeinduced structural pounding,” Earthquake Engineering & Structural Dynamics, vol. 34, no. 6, pp. 595–611, 2005. View at: Publisher Site  Google Scholar
 T. Hughes, The Finite Element Method—Linear Static and Dynamic Finite Element Analysis, Prentice Hall, Inc., Upper Saddle River, NJ, USA, 1987.
 L. Q. Hong, L. Ying, L. Hao, H. G. Hu, and Q. D. Hu, “Seismic response characteristics of stabilizing pile based on elasticplastic analysis,” Shock and Vibration, vol. 2018, Article ID 7672587, 15 pages, 2018. View at: Publisher Site  Google Scholar
 S. A. Anagnostopoulos and K. V. Spiliopoulos, “An investigation of earthquake induced pounding between adjacent buildings,” Earthquake Engineering & Structural Dynamics, vol. 21, no. 4, pp. 289–302, 1992. View at: Publisher Site  Google Scholar
 J. Azevedo and R. Bento, “Design criteria for buildings subjected to pounding,” in Proceedings of the Eleventh World Conference on Earthquake Engineering, Acapulco, Mexico, June 1996. View at: Google Scholar
 R. Jankowski, “Nonlinear viscoelastic model of structural pounding,” in Proceedings of the 13th World Conference on Earthquake Engineering, pp. 1–6, Vancouver, Canada, August 2004. View at: Google Scholar
 E. L. Wilson, ThreeDimensional Static and Dynamic Analysis of Structures, Computers and Structures, Inc., Berkeley, CA, USA, 2002.
 H. Hao, C. S. Oliveira, and J. Penzien, “Multiplestation ground motion processing and simulation based on SMART1 array data,” Nuclear Engineering and Design, vol. 111, no. 3, pp. 293–310, 1989. View at: Publisher Site  Google Scholar
 D. S. Wang, Q. M. Feng, and G. X. Wang, “Analysis model of pounding between adjacent bridge girders during earthquakes based on collinear compact between rod theory,” Engineering Mechanics, vol. 21, no. 2, pp. 157–166, 2004, in Chinese. View at: Google Scholar
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