Shock and Vibration
Volume 2021 (2021), Article ID 6644158, 14 pages
https://doi.org/10.1155/2021/6644158

Research Article

Comparison of Dynamic Responses of Parallel-Placed Adjacent High-Rise Buildings under Wind and Earthquake Excitations

Huaxiao Wu,¹ Qinhua Wang,² Nayan Deep Tiwari,¹ and Dario De Domenico³

¹Department of Civil and Environmental Engineering, Shantou University, Shantou 515063, China
²School of Civil Engineering and Architecture, Southwest University of Science and Technology, Mianyang 621010, China
³Department of Engineering, University of Messina, Messina 98166, Italy

Correspondence should be addressed to Qinhua Wang; qinhuawang@stu.edu.cn

Received 4 November 2020; Revised 3 May 2021; Accepted 12 June 2021; Published 28 June 2021

Academic Editor: Salvatore Caddemi

Copyright © 2021 Huaxiao Wu et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

Abstract.

Two parallel-placed adjacent high-rise buildings are often linked to each other through passive control devices for vibration mitigation purposes. The mitigation efficiency of these control devices mainly depends on the characteristics of relative dynamic responses, namely, opposite-sign and same-sign responses of the two buildings. The present research first identifies an opposite-sign response factor to estimate the time ratio of opposite-sign responses. Subsequently, a structure comprising two adjacent high-rise buildings (with different natural frequency ratios) subjected to both wind and earthquake excitations is analyzed. Wind-induced responses are evaluated based on wind loads obtained from wind tunnel tests, while earthquake responses are determined through a suite of 44 natural ground-motion records. The results indicate that opposite-sign factors of the displacement, velocity, and acceleration responses under wind loads, especially at across-wind direction, are larger than those under earthquake excitations, and opposite-sign response factors under wind loads are insensitive to variation of the natural frequency ratio of the two adjacent buildings compared with those under earthquake excitations. The conclusions of this research may be helpful for wind-resistant and antiseismic design of parallel-placed adjacent high-rise buildings.

1. Introduction

With the rapid development of metropolitan cities over the years, high-rise buildings are often constructed in close proximately to each other [1]. Some notable examples of such attractive building systems include the Petronas Twin Towers in Kuala Lumpur, the Marina Bay Sands Hotel, American Coopers in New York, and many more. These slender parallel-placed adjacent high-rise buildings are sensitive to dynamic excitations [2–4]. When these buildings are located in regions prone to hurricanes and earthquakes simultaneously, they may suffer from significant damage in their uncontrolled configurations. Hence, various passive control devices may be installed on these buildings to simultaneously control undesirable excessive dynamic responses induced by wind loads and earthquake excitations [5–7].

In order to design and install passive control devices accurately, characteristics of dynamic responses of parallel-placed adjacent high-rise buildings under wind and earthquake excitations should be investigated to simultaneously control wind- and earthquake-induced vibrations. Unlike earthquake excitations, wind loads acting on the adjacent high-rise buildings may be more complicated [8]. The reason can be mainly attributed to the following two facts: (1) due to the complex interaction of wind and exterior shape of buildings, wind loads include along-wind and across-wind components, which are mainly generated by incoming turbulence and vortex-shedding, respectively [9], and (2) wind loads acting on the target building can be strongly affected by aerodynamic interference if surrounding buildings exist [10–12]. Currently, most of the literature studies are focused on the assessment of structural safety under independent hazards i.e., under earthquakes [13–18] or strong winds [19–22]. However, research interests have been developed amongst engineers and researchers to investigate the design of structures under a combination of extreme multiple hazards [23]. Vulcano [24] investigated the dynamic responses of a single building with base-isolated devices subjected to strong wind loads and earthquake excitations to pursue the optimal design of the base-isolation system. Hong and Gu [25] found that, in the case of tall flexible buildings whose lateral forces are mainly governed by wind loads, the combined loads after considering wind loads and earthquake excitations may be more unfavourable as compared with those involving wind loads in seismic design. Duthinh and Simiu [26] developed a design approach for buildings in regions where strong winds and earthquakes are significant while satisfying the minimum requirements in design standards. Mahmoud and Cheng [27] proposed a probabilistic framework for estimating the lifecycle cost for two steel buildings subjected to different seismic and wind intensities. Zheng et al. [28] presented a multi-hazard-based framework to assess the damage risk of high-rise buildings subjected to wind and earthquake hazards simultaneously. A comparative study of dynamic responses of liquid storage tanks under wind, earthquake, and combined wind and earthquake excitations is presented by Jing et al. [29]. Their results showed that under strong winds the dynamic responses of the liquid storage tank under wind loads alone are larger than those under earthquake excitations, and the dynamic responses under wind-earthquake interaction are larger than those under wind and earthquake excitations alone. Xu et al. [30] proposed an analytical model for an isolated high-rise building with friction pendulum bearing and magnetorheological damper to reduce dynamic responses under combined wind loads and earthquake excitations. Roy and Matsagar [31] investigated the combined wind and earthquake hazards effects on the failure probability of multistorey steel buildings equipped with passive control devices. Most of the aforementioned studies focused on dynamic responses or failure evaluation of a single building under the simultaneous action of wind and earthquake.

To the best of the authors’ knowledge, the comparison between the dynamic responses of adjacent high-rise buildings subjected to wind loads and earthquake excitations has not been thoroughly investigated in the literature. Hence, in the present study, an attempt has been made to investigate the dynamic response characteristics of these parallel-placed linked high-rise buildings to control the structural vibrations under strong wind and earthquake excitations. The present study is arranged as follows: firstly, the equations of motion for the adjacent buildings under the two different kinds of dynamic excitations are established. Subsequently, a structure comprising two adjacent high-rise buildings is briefly introduced considering wind loads obtained from wind tunnel tests and natural earthquake records. Finally, an opposite-sign response factor is identified to compare the displacement, velocity, and acceleration responses of the linked adjacent buildings with different natural frequency ratios under wind loads and earthquake excitations.

2. Mathematical Model of the Adjacent Buildings under Wind and Seismic Excitations

A lumped-mass sketch of adjacent high-rise buildings is shown in Figure 1. The two buildings, named Building 1 (i storeys) and Building 2 (j storeys), are linked by a corridor with rigid support at one terminal and sliding support at the other terminal. Different passive control devices may be installed at the storey having the same intermediate height as that of the corridor to mitigate the dynamic responses when these responses do not satisfy the requirement of design standards. These different types of passive control devices can be categorized into displacement-dependent such as metal friction dampers [32, 33] or buckling-restrained braces [34], velocity-dependent such as fluid viscous dampers [35–39], or acceleration-dependent primarily related to inerter devices [40–42]. Therefore, while selecting suitable passive control devices, the dynamic response characteristics of the adjacent high-rise buildings under wind loads and seismic excitations should be fully considered to obtain a better mitigation efficiency of these devices.

Figure 1: The structural sketch of the two adjacent high-rise buildings.

The equations of motion of adjacent high-rise buildings without any passive control devices under wind loads and seismic excitations can be expressed as in equations (1) and (2), respectively.

where, , , and are the mass, damping, and stiffness matrices of the two adjacent high-rise buildings, respectively. The lumped mass and lateral stiffness of each storey can be obtained from the finite element model of the buildings. , , and correspond to the acceleration, velocity, and displacement column vectors of adjacent high-rise buildings, respectively. is the wind load vector acting on the center of mass of each storey, which can be obtained from wind tunnel tests of synchronous multipoint pressure measurements. is the acceleration of ground motion at time , and is a column vector with entries, in which all entries are equal to 1.

The mass matrix can be expressed as

where and denote the dead and live loads (properly combined with each other) of the storey of Building 1 and the storey of Building 2, respectively.

The stiffness matrix can be defined as

where and represent the stiffness matrix of original Building 1 and Building 2, respectively.

The damping matrix C can be expressed according to the Rayleigh formulation:

where and are two scalar coefficients of proportionality.

Since the mass, damping, and stiffness matrices are orthogonal to the mode shape, equations (1) and (2) can be decoupled into the modal coordinates as expressed in equations (6) and (7), respectively.

where , , , , , and denote the order generalized coordinates, damping ratio, natural circular frequency, generalized aerodynamic force, and generalized mass, vibration mode, respectively. The superscript T denotes the transpose operator, and the modal participation coefficient is defined as

The time-domain integration method, i.e., Duhamel’s integral, is used to solve the generalized coordinate under wind and earthquake excitations, which are formulated as in equations (9) and (10), respectively.

where is the damped natural frequency of the structure.

According to the modal superposition method, the displacement response of the structure at arbitrary t can be expressed as

where is the number of the mode shape involved while calculating the displacement time history of the structure.

3. Case Study

The following section introduces a case study of two adjacent high-rise buildings and the related excitations to evaluate the dynamic responses: in particular, wind loads are obtained from wind tunnel tests of synchronous multipoint pressure measurements, while 44 natural ground-motion records are considered for earthquake-induced excitations.

3.1. A Brief Introduction of the Two Adjacent High-Rise Buildings

The same structure previously considered by De Domenico et al. [43] is analyzed as a case, comprising two adjacent high-rise buildings whose main properties are summarized as follows. Building 1 has 59 storeys with 268 meters height and Building 2 consists of 55 storeys with a height of 210.2 meters. The main dimensions of the adjacent buildings and the definition of the coordinate system for structural analysis and wind directions are shown in Figures 2(a) and 2(b).

(a)

(b)

Figure 2: (a) Plane view of adjacent buildings and definition of the coordinate system and wind direction [8] and (b) axonometric sketch of two buildings [43].

The distribution of lumped masses of the two buildings is presented in Figure 3(a)The lateral stiffness along the x-axis of two buildings is smaller than that along the y-axis; as a result, the most unfavourable dynamic response will probably occur along the x-axis. Hence, only lateral stiffness along the x-axis is plotted in Figure 3(b).

(a)

(b)

Figure 3: Distribution of (a) lumped masses and (b) lateral stiffness of the two buildings along the x-axis [44].

According to the mass and stiffness matrices of the individual adjacent buildings, the fundamental frequencies of Building 1 and Building 2 are obtained. The first five natural frequencies of the individual buildings are listed in Table 1. As shown in Table 1, the natural frequency ratio (NFR) which is defined as the ratio of the first natural frequency of Building 1 to that of Building 2 can be estimated as 0.86/1. To investigate the effects of natural frequency ratio on dynamic responses of adjacent buildings under different excitations, the mass of Building 2 is adjusted so as to make its first natural frequency equal to that of Building 1, which means that the natural frequency ratio is equal to 1/1.

Table 1: Natural frequencies of individual buildings.

Frequency (Hz)
f₁
f₂
f₃
f₄
f₅

Building 1
0.139
0.347
0.554
0.756
0.959

Building 2
0.161
0.399
0.636
0.866
1.090

3.2. Wind Tunnel Test and Ground-Motion Time Histories

Wind tunnel tests of synchronous multipoint pressure measurement are carried out in the wind tunnel laboratory of Shantou University. The scale ratio of the test model to the prototype of the buildings is 1 : 300. In the wind tunnel tests, the B-type wind field is simulated according to the Chinese building code [45]. The wind tunnel tests are conducted for 24 wind directions ranging from 0° to 345° at an interval of 15° to investigate the effect of wind direction on the dynamic responses of the structure. For the displacement and acceleration responses of the buildings, the basic wind pressures are assumed to be 0.6 kPa and 0.35 kPa (corresponding to 50-year and 10-year return periods, respectively). More detailed information about the wind tunnel test can be found in the literature [44].

Based on the results obtained from wind tunnel tests, the normalized power spectral density (PSD) of base shear forces on Building 1 and Building 2 at across-wind direction is plotted in Figure 4. The PSD curves of Building 1 and Building 2 have obvious peaks corresponding to the dimensionless values  = 0.107 and 0.120, where represents frequency measuring by Hz, B is width of the individual building, denotes mean wind speed at top of the buildings corresponding to 50-year return period, and and represent self-power spectrum and root mean square of the base shear forces, respectively.

Figure 4: Normalized PSD of base shear forces at the across-wind direction.

With regard to the earthquake excitation, the dynamic responses of adjacent high-rise buildings are evaluated under 44 natural ground-motion records, which are two horizontal components of 22 earthquakes obtained from the FEMA P-695 far-field record set [46]. Some seismological information of the 22 earthquakes is listed in Table 2. These ground-motion records have been used in previous researches to investigate the mitigation effects of different passive control devices [47, 48]. The individual and average PSDs of 44 recorded earthquakes are shown in Figure 5. It is observed that the predominant frequencies of these earthquake excitations concentrate on a higher frequency range as compared to those of wind loads as shown in Figure 4.

Table 2: Information of 22 considered earthquakes from FEMA P-695 far-field record set [46].

ID no.
Earthquake
Recording station

Magnitude
Year
Name
Name
Owner

1
6.7
1994
Northridge
Beverly Hills-Mulhol
USC

2
6.7
1994
Northridge
Canyon Country-WLC
USC

3
7.1
1999
Duzce, Turkey
Bolu
ERD

4
7.1
1999
Hector Mine
Hector
SCSN

5
6.5
1979
Imperial Valley
Delta
UNAMUCSD

6
6.5
1979
Imperial Valley
El Centro Array #11
USGS

7
6.9
1995
Kobe, Japan
Kobe, Japan
CUE

8
6.9
1995
Kobe, Japan
Shin-Osaka
CUE

9
7.5
1999
Kocaeli, Turkey
Duzce
ERD

10
7.5
1999
Kocaeli, Turkey
Arcelik
KOERI

11
7.3
1992
Landers
Yermo Fire Station
CDMG

12
7.3
1992
Landers
Coolwater
SCE

13
6.9
1989
Loma Prieta
Capitola
CDME

14
6.9
1989
Loma Prieta
Gilroy Array #3
CDMG

15
7.4
1990
Manjil, Iran
Abbar
BHRC

16
6.5
1987
Superstition Hills
El Centro Imp. Co.
CDMG

17
6.5
1987
Superstition Hills
Poe Road (Temp)
USGS

18
7.0
1992
Cape Mendocino
Rio Dell Overpass
CDMG

19
7.6
1999
Chi-Chi, Taiwan
CHY101
CWB

20
7.6
1999
Chi-Chi, Taiwan
TCU045
CWB

21
6.6
1971
San Fernando
LA-Hollywood Stor
CDMG

22
6.5
1976
Friuli, Italy
Tolmezzo
--

Figure 5: The individual and mean PSDs of the 44 recorded earthquakes belonging to the FEMA P695 far-field record set [40].

4. Dynamic Response Analysis of Adjacent Buildings under Wind and Earthquake Excitations

According to the mathematical model described in Section 2, wind loads and earthquake excitations in Section 3, the time history of displacement, velocity, and acceleration response for the adjacent high-rise buildings under wind loads and seismic excitations are estimated numerically. To quantitatively compare these response characteristics, an opposite-sign response factor is introduced in this study, which is defined as

where is the sum of the time intervals during which fluctuating components of wind-induced displacement responses or, similarly, total velocity and acceleration responses of buildings (the mean values of velocity and acceleration responses are equal to zero) have opposite sign, and is the total statistical time of dynamic responses.

4.1. Comparison of Displacement Responses

According to equation (1) to equation (11), the time histories of dynamic displacement responses of adjacent high-rise buildings under wind loads and earthquake excitations are evaluated. The total wind-induced responses of structures can be decomposed into mean value and fluctuating components. Previous literature [8, 43, 44, 49, 50] showed that the passive control devices can only suppress the fluctuating vibration, thus while investigating dynamic response characteristics, only the fluctuating response is analyzed. For the clarity of the figures, Figure 6 shows only the 50-second segment of fluctuating displacement time history of the adjacent high-rise buildings and the shaded part indicates that the direction of displacement of the two buildings is opposite; i.e., if the sign of one response is negative, the other sign is positive. Figures 6(a)–6(c) illustrate the time history of the wind-induced fluctuating displacement responses at the height of 210.2 meters of the adjacent buildings with a natural frequency ratio of 0.86/1 at 0°, 90°, and 180° wind directions, respectively. Figure 6(d) presents the time history of displacement for the adjacent buildings at the height of 210.2 meters under the No. 10 earthquake excitation.

(a)

(b)

(c)

(d)

Figure 6: Time histories of displacement responses at 210.2 m height under (a) 0° wind direction, (b) 90° wind direction, (c) 180° wind direction, and (d) the No. 10 earthquake excitation.

Once the time histories of wind-induced and earthquake-induced displacement responses are obtained, the opposite-sign displacement factor of the adjacent buildings at the height of 210.2 meters may be estimated according to equation (12). The total statistical time for seismic responses is the same as recorded time of each ground motion, while that of wind-induced responses is set to be 600 seconds. The variations of opposite-sign displacement factor with wind directions and different seismic excitations are shown in Figure 7. The red dashed line in the figure represents the mean value of factors of wind directions and earthquake excitations, respectively. Figure 7(a) indicates that wind-induced opposite-sign displacement factor hardly varies with wind directions, while it is nearly not affected by the natural frequency ratio. Figure 7(b) indicates that the opposite-sign factor of the two buildings with the natural frequency ratio of 0.86/1 is much larger than that with the natural frequency ratio of 1/1 under the majority of seismic excitations. The mean value (for all the 44 seismic records) of the opposite-sign displacement response factor is 36.5% when the natural frequency ratio is 0.86/1, and it is reduced to 11.1% when the natural frequency ratio is 1/1.

(a)

(b)

Figure 7: Variation of opposite-sign displacement factor at 210.2 m height under (a) 24 wind directions and (b) 44 earthquake excitations.

Figure 8 shows the variation of opposite-sign displacement factor with the height of buildings under wind and seismic excitations. Figure 8(a) indicates that the factors under the four wind directions do not vary significantly with the height of the buildings and are insensitive to the natural frequency ratio. Figure 8(b) illustrates that the mean value of the opposite-sign factor of the two buildings subjected to seismic excitations is much smaller when the natural frequency ratio is equal to 1/1 than that when the natural frequency ratio is equal to 0.86/1 at any height of the two buildings.

(a)

(b)

Figure 8: Variation of opposite-sign displacement factor with height of buildings under (a) wind loads and (b) 44 earthquake excitations.

4.2. Comparison of Velocity Responses

The velocity response time histories can be obtained from the derivative of the displacement time histories with respect to time. Figures 9(a)and 9(b) show the time histories of velocity response at a height of 210.2 meters of the two buildings with the natural frequency ratio being 0.86/1 under across-wind direction (90°) and the No. 10 seismic excitation, respectively. The shaded part in Figure 9 means that the velocity responses of the two buildings have the opposite sign.

(a)

(b)

Figure 9: Time histories of velocity responses at 210.2 m height under (a) 90° wind direction and (b) the No. 10 earthquake excitation.

The variations of the opposite-sign velocity factor with different wind directions and earthquake excitations are shown in Figure 10. Figure 10(a) indicates that the wind-induced velocity factors are insensitive to wind directions and natural frequency ratios of the two buildings since all the values of factors approach around 50% under 24 wind directions and different natural frequency ratios. Figure 10(b)illustrates that factors related to velocity responses under seismic excitations are sensitive to natural frequency ratio of the two buildings. Under most of the seismic excitations, the factors are relatively lower when the natural frequency ratio is 1/1 than that at the condition of the natural frequency ratio being 0.86/1. The mean values of the opposite-sign factors for seismic excitation are 40.3% and 25.0% corresponding to natural frequency ratios of 0.86/1 and 1/1, respectively.

(a)

(b)

Figure 10: Variation of opposite-sign velocity factor at 210.2 m height under (a) 24 wind directions and (b) 44 earthquake excitations.

Figure 11 presents the variation of the opposite-sign velocity factor with the varying height of the two buildings under wind loads and earthquake excitations, respectively. Figure 11(a) illustrates that the factors remain steady with the varying height and natural frequency ratio of the two adjacent buildings, and these values of factors lie around 50% at the four typical wind directions. Figure 11(b) indicates that the mean value of the velocity factor of the two buildings in the case of natural frequency being 0.86/1 is larger than that when natural frequency ratio is 1/1 at any height of the two buildings under seismic excitations.

(a)

(b)

Figure 11: Variation of opposite-sign velocity factor with height of buildings under (a) wind loads and (b) 44 earthquake excitations.

4.3. Comparison of Acceleration Responses

The acceleration response time histories of the adjacent buildings under wind loads and seismic excitations are estimated in this section. Figures 12(a) and 12(b) show a 50-second time history of acceleration responses of the two buildings under the across-wind direction (90°) and the No. 10 earthquake excitation respectively.

(a)

(b)

Figure 12: Time histories of acceleration responses at 210.2 m height under (a) 90° wind direction and (b) the No. 10 earthquake excitation.

Figure 13 shows the variation of the opposite-sign acceleration response factor with different wind directions and earthquake excitations. Figure 13(a) indicates that the wind-induced acceleration response factor remains almost invariant while changing wind directions and natural frequency ratio of adjacent buildings, and the mean value for all wind directions in each working condition still lies around 50%. As for earthquake excitations, Figure 13(b) demonstrates that the variation of the earthquake-induced acceleration response factors caused by the changes in natural frequency ratio is not as significant as that of the displacement or velocity response factor shown in Figures 7(b)and 10(b), respectively. The mean value of the opposite-sign acceleration response factor under the 44 earthquake excitations is 40.6% when the natural frequency ratio is 0.86/1, while the factor is 40.3% when natural frequency ratio equals to 1/1.

(a)

(b)

Figure 13: Variation of opposite-sign acceleration factor at 210.2 m height under (a) 24 wind directions and (b) 44 earthquake excitations.

Figure 14 presents the variation of opposite-sign acceleration response factor with the height of two buildings under wind and seismic excitations. Figure 14(a) shows that the acceleration response factors are almost unaffected with the changing height of the building and natural frequency ratios of the two buildings at the four wind directions, which is similar to the variation of wind-induced velocity response factor with height as shown in Figure 11(a). With regard to the seismic excitation, Figure 14(b) indicates that the acceleration response factors at the top storeys of the adjacent buildings with natural frequency ratio of 1/1 are equal to the case when natural frequency ratio is 0.86/1.

(a)

(b)

Figure 14: Variation of opposite-sign acceleration factor with height of buildings under (a) wind loads and (b) 44 earthquake excitations.

5. Conclusion and Discussion

In the present work, an opposite-sign response factor is proposed to compare the characteristics of the dynamic responses of two adjacent high-rise buildings under wind loads and earthquake excitations, respectively. This factor is defined as the ratio between the time duration during which dynamic responses of the adjacent buildings have the opposite sign and the total statistical time of dynamic responses. The following conclusions are obtained as a result of the present research.

(1)For fluctuating displacement responses, the opposite-sign displacement response factors vary more significantly with different earthquake excitations than that under different wind directions. Besides, these factors of seismic excitations are more sensitive to changes in the natural frequency ratio of the two buildings as compared to wind loads.(2)In terms of the velocity responses, the opposite-sign velocity response factors remain almost constant with change in both wind directions and the natural frequency ratio of the two buildings, under wind loads. However, under earthquake excitations, these factors vary with different earthquake records and natural frequency ratios. Furthermore, the mean value of the wind-induced factor is larger than that obtained under 44 seismic factors.(3)Regarding acceleration responses, results of wind-induced opposite-sign acceleration factors are similar to those of wind-induced velocity responses, and the mean values of wind-induced acceleration factors are also larger than those of 44 seismic excitations. Nevertheless, the seismic acceleration factors do not vary significantly with different earthquake records and natural frequency ratios as compared to that of seismic displacement and velocity responses.

In general, the opposite-sign dynamic response factors of the adjacent buildings under the action of wind loads are larger than those under earthquake excitations. This result implies that when inter-building passive control devices are installed to mitigate dynamic responses of the two adjacent high-rise buildings, the mitigation efficiency of the devices for wind-induced vibration control is better than the seismic vibration control. This anticipation is consistent with the previous works [8, 43, 44, 48] from the authors dealing with wind-induced and earthquake-induced vibration mitigation with inter-building passive control devices. In these researches, different acceleration-dependent tuned inerter dampers, i.e., TMDI and TLCDI, were employed to control wind-induced and seismic responses of the two adjacent high-rise buildings analyzed in the present work. After the installation of TMDI on the two adjacent buildings, the mean reduction coefficients of the top-level acceleration are 37.5% for Building 1 and 45.2% for Building 2 at the across-wind direction, while the maximum corresponding reduction coefficients under seismic excitations are only 23.0% and 37.5% [43, 44]. If TLCDI is installed to mitigate dynamic responses, the reduction coefficients of wind-induced acceleration responses of Building 1 and Building 2 are 37.7% and 42.0%, respectively, while the corresponding reduction coefficients in case of seismic acceleration control are only 15.7% and 26.1% [8, 48]. These findings verify that both TMDI and TLCDI are more effective in controlling the wind-induced acceleration responses of adjacent high-rise buildings, as compared to earthquake-induced acceleration responses. Hence, the opposite-sign response factor analyzed in this study could be regarded as an applicable and reasonable indicator to evaluate the mitigation efficiency of passive control devices even prior to their installation.

Data Availability

The data used to support the findings of this research are available from the corresponding author upon request.

Conflicts of Interest

The authors declare that they have no conflicts of interest.

Acknowledgments

This research was supported by Key Laboratory of Structure and Wind Tunnel of Guangdong Higher Education Institutes.

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