Bearing Behavior of H-Shaped Honeycombed Steel Web Composite Columns with Rectangular Concrete-Filled Steel Tube Flanges under Eccentrical Compression Load

College of Civil and Architectural Engineering, Northeast Petroleum University, Heilongjiang Key Laboratory of Disaster Prevention, Mitigation and Protection Engineering, No. 99 Xuefu Road, Longfeng District, Daqing 163318, China Key Laboratory of Earthquake Engineering and Engineering Vibration, Institute of Engineering Mechanics, China Earthquake Administration, No. 29 Xuefu Road, Nangang District, Harbin 150000, China Handan Key Laboratory of Building Physical Environment and Regional Building Protection Technology, School of Architecture and Art, Hebei University of Engineering, No. 19 Taiji Road, Handan Economic and Technological Development District, Handan 056038, China


Introduction
H-shaped honeycombed steel web composite columns with rectangular concrete-filled steel tube flanges (STHCCs) are types of novel composite members formed by connecting two concrete-filled rectangular steel tubular flanges with a honeycombed steel web. e core concrete can prevent and delay the local buckling of the steel tube and the instability failure of the specimens effectively, and on the other hand, the confinement of the steel tube makes the core concrete in a state of triaxial compression, which can effectively improve the capacity of resisting deformation and the compressive strength of the core concrete. In particular, the honeycombed steel web connects the two limbs into an organic whole, which can not only reduce the weight of the structure, but also improve the stiffness and bearing capacity of the composite columns. ese types of composite columns are characterized by high ultimate bearing capacity, good ductility, and excellent stability bearing capacity, which are superior to ordinary concrete-filled steel tube (CFST) columns and honeycombed columns [1].
Numerous research studies regarding CFSTcolumns and honeycombed columns have been carried out at home and abroad. Jayaganesh et al. [2] conducted tests on 6 square and 6 circular CFST short columns to study the influence of concentric local compression on the structural behavior of CFST columns under axial compression. Ahmed et al. [3] proposed a simplified model of concrete-filled square steel tube columns subjected to axial compression and presented the interaction curve of high-strength square concrete-filled double steel tubular (CFDST) under eccentric loading by establishing the buckling model of CFDST under axial compression and uniaxial bending. Vatulia et al. [4] analyzed the deformation development regularity of concretefilled rectangular steel tube columns with different lengths subjected to eccentrical loading through the integral method and established the calculation mathematical model of eccentrical compression bearing capacity for concrete-filled rectangular steel tube columns. Yu et al. [5] put forward the formula of eccentrical compression bearing capacity of recycled coarse aggregate self-compacting CFST columns based on the experimental studies and analyzed the applicability of the formula in the United States, China, and Japan. Li et al. [6] conducted eccentrical compression tests of L-shaped square CFST columns and established a finite element (FE) model to study the eccentrical compression behavior of this type column and proposed a bearing capacity analysis method of the rectangular concrete-filled stainless steel tubular (CFSST) columns based on the stress yield criterion at the edge of the section base. Rong et al. [7] analyzed the eccentrical compression behavior of concretefilled square steel tube columns with I-shaped CFRP through experimental research and FE simulation, and derived the calculation formula of eccentrical compression bearing capacity of composite columns. Sui et al. [8] investigated the failure mode of 19 multi-element composite T-shaped CFST columns under biaxial eccentrical compression and proposed the simplified calculation formula of eccentrical compression bearing capacity. Chen et al. [9] studied the influence regularity of different parameters on eccentrical compression test of 18 concrete-filled square steel tube columns with spiral stirrups and derived the calculation formula of eccentrical compression bearing capacity of these types of columns. Twenty-one recycled self-compacting concrete-filled circular steel tubular (RSCFCST) columns were tested subjected to eccentric compression by Yu et al. [10], and bearing capacity of these kinds of composite columns under eccentric compression was obtained systemically; finally, an analytical model for predicting the effective stiffness of RSCFCST columns under eccentric compression was proposed based on the moment magnifier method. In 2017, Ji et al. [11] investigated the eigenvalue buckling behavior of 29 STHCCs by ABAQUS software. Based on this, in 2018, Ji et al. [12] carried out the research on the overall nonlinear stability of STHCCs and derived the calculation expression of nonlinear stability bearing capacity of STHCCs. In the same year, in order to investigate the influence regularity of different parameters on the axial compression bearing capacity of STHCCs, Ji et al. [13,14] designed and conducted the axial compression tests of 16 short STHCCs and proposed the calculation expression of axial compression bearing capacity for STHCCs. In 2020, Ji et al. [15] studied the eccentrical compression behavior of 17 reduced-scale STHCCs by ABAQUS software and derived the calculation expression of eccentrical compression bearing capacity of reduced-scale STHCCs.
At present, the research on STHCCs is mainly aimed at axial compression and stability behavior, and few studies have been performed on the eccentrical compression behavior of such full-scale columns. Based on the existing axial compression test and results of reduced-scale eccentrical compression behavior of STHCCs, the numerical simulation analysis of 33 full-scale STHCCs is further carried out by ABAQUS software. e influence of different parameters on the ultimate bearing capacity of these types of full-scale composite columns under eccentrical compression is discussed. e calculation formula of eccentrical compression bearing capacity of these types of columns can be obtained by statistical regression based on the simulation results, which can provide technical support for the subsequent research and application of these types of columns.

Specimens Design
In order to investigate the mechanical behavior of full-scale H-shaped honeycombed steel web composite columns with rectangular concrete-filled steel tube flanges (STHCCs) under eccentrical compression, 33 full-scale STHCCs were designed with the eccentricity (e), the slenderness ratio (λ), the cubic compressive strength of concrete (f cuk ), the thickness of the steel tube flange (t 1 ), the thickness of honeycombed steel web (t 2 ), diameter-depth ratio (d/h w ), space-depth (s/h w ), and the yield strength of the steel tube (f y ) as the main parameters. e schematic diagram and specific parameters of the specimens are shown in Figure 1 and Table 1, where h w represents the width of webs, d refers to the diameter of the honeycombed holes on the web, and s represents the distance between two honeycombed holes.

Constitutive Model for Materials
e stress-strain curve of steel consists of five stages of elastic, elastic-plastic, plastic, strengthening, and second plastic flow.
irty-three STHCCs designed are all medium-long columns; hence, the strengthening stage of steel can be neglected.
e ideal elastoplastic constitutive model is applied to characterize the elastoplastic behavior of steel, as shown in Figure 2(a). Poisson's ratio of steel is set as 0.3.

Constitutive Model for Concrete.
Han [16], Pagoulatou et al. [17], Teng et al. [18], Mander et al. [19], and Qian et al. [20] have successively given the constitutive models of confined concrete, and the constitutive model of unconfined concrete has been given in the Chinese Code for Design of Concrete Structures (GB50010-2010) [21]. e comparisons of different constitutive models are illustrated in Figure 2 rough comparative analysis, the constitutive model proposed by Han [16], which considered the confinement effect, is applied in this article. It can be seen that the ductility of concrete is improved significantly; nevertheless, the strength of concrete remains unchanged. e following formula represents the stress-strain curve of concrete under uniaxial compression: e following formula represents the stress-strain curve of concrete under uniaxial tensile: 1σ p , and other variables can be found in reference [16].

Modeling Process and Boundary Conditions.
e FE models of STHCCs were established by ABAQUS software [22], as shown in Figure 3. By adding material properties and then assigning material properties to the members, the constitutive model proposed by Han can be input into the material of ABAQUS. e eight-joint hexahedral elementtype C3D8R was used to simulate the rectangular steel tube, honeycomb steel web, and concrete. e nonlinear symmetrical contact between steel tube and concrete was simplified as normal hard contact and tangential friction contact, and the Coulomb friction coefficient (μ) [23] was set as 0.25. Two reference points were set at the center of the upper and lower surfaces of the columns, namely, RP1 and RP2. e reference points were, respectively, coupled with the top end and the bottom end of the columns. e displacements (U x , U y, UR x , UR y ) of the top end for columns were constrained by RP1, and the displacements (U x , U y , U z , UR x , UR y ) of the bottom end for columns were constrained by RP2.

Experimental Verification of FE Models
In order to verify the rationality of the FE models, numerical simulation analysis on 4 specimens selected from reference [24] and 11 specimens selected from references [25][26][27][28] was carried out, as shown in Table 2. e load-lateral deflection curves of the mid-span sections and failure modes were obtained. By the comparison, it could be seen from Figure 4 that the curves obtained by the simulation were consistent with the test curves. e comparisons of the bearing capacity obtained by simulation (N a ) and the bearing capacity by test (N t ) were shown in Figure 5. e maximum error was 8.74%, which could meet the requirements of engineering accuracy. e rationality of FE modeling proposed in this article was verified.

Load-Vertical Displacement Curves.
e load (N)-vertical displacement (Δ) curves of the specimens with different eccentricity, slenderness ratio, and diameter-depth ratio are shown in Figure 6. It can be found that the load (N)-vertical displacement (Δ) curves can be classified into four development stages: elastic stage, elastic-plastic ascending stage, descending stage, and gentle stage. With the increase in the eccentricity, the slenderness ratio, and diameter-depth ratio, the eccentrical compression bearing capacity of the specimens gradually decreases. Figure 6(a) shows the load (N) versus the vertical displacement (Δ) relationships of the specimens with different eccentricity, and when the eccentricity of the specimens increases from 80 mm to 400 mm, the initial stiffness of the specimens decreases from 5.06 × 10 6 kN/m to 1.97 × 10 6 kN/m, which reduce by 61.1%. e eccentrical compression capacity of the specimens decreases from 17.39 × 10 3 kN to 9.9 × 10 3 kN, which decreases by 42.6%. It indicates that with the increase in the eccentricity, the initial stiffness and eccentrical compression capacity of the specimens decrease. Figure 6(b) shows the load (N) versus the vertical displacement (Δ) relationships of the specimens with different slenderness ratio, in which as the slenderness ratio of the specimens increases from 19.4 to 60.97, the initial stiffness of the specimens decreases from 3.62 × 10 6 kN/m to 1.17 × 10 6 kN/m, which reduces by 67.7%. e eccentrical compression capacity of the specimens decreases from 12.86 × 10 3 kN to 10.88 × 10 3 kN, which decreases by 15.4%, while the decline section of the curves gradually slow down. It indicates that with the increase in the slenderness ratio, the initial stiffness and eccentrical compression capacity of the specimens decrease, whereas the ductility increases. Figure 6(c) shows the load (N) versus the vertical displacement (Δ) relationships of the specimens with different diameter-depth ratio, and when the diameterdepth ratio of the specimens increases from 0.1 to 0.75, the eccentrical compression capacity of the specimens decreases from 13.61 × 10 3 kN to 11.87 × 10 3 kN, which decreases by 12.8%, while the decline section of the curves gradually slow down. It can be seen that with the increase in the Test curve (Y.S. Du [24][25][26][27]) Simulation curve    Advances in Civil Engineering diameter-depth ratio, the eccentrical compression bearing capacity of the specimens decreases gradually. Figure 7 illustrates the load (N) versus the vertical displacement (Δ) relationships of the specimens with different parameters. Obviously, with the increase in the cubic compressive strength of concrete, the thickness of the steel tube flange, the thickness of honeycombed steel web, spacedepth ratio, and the yield strength of the steel tube, the eccentrical compression bearing capacity of the specimens increases gradually. Figure 7(a) shows the load (N) versus the vertical displacement (Δ) relationships of the specimens with different cubic compressive strength of concrete, and when the cubic compressive strength of concrete increases from 30 MPa to 70 MPa, the eccentrical compression capacity of the specimens increases from 11.05 × 10 3 kN to 17.45 × 10 3 kN, which raises by 57.92%. It indicates that with the increase in the cubic compressive strength of concrete, the eccentrical compression capacity of the specimens increases. Figure 7(b) shows the load (N) versus the vertical displacement (Δ) relationships of the specimens with different thickness of the steel tube flange, and when the thickness of the steel tube flange increases from 6 mm to 14 mm, the eccentrical compression capacity of the specimens increases from 11.37 × 10 3 kN to 16.32 × 10 3 kN, which raises by 43.54%. It reflects that with the increase in the thickness of the steel tube flange, the eccentrical compression capacity of the specimens increases. e load (N) versus the vertical displacement (Δ) relationships of the specimens with different thickness of honeycombed steel web are illustrated in Figure 7(c), and when the thickness of honeycombed steel web increases from 8 mm to 16 mm, the eccentrical compression capacity of the specimens increases from 12.38 × 10 3 kN to 13.35 × 10 3 kN, which increases by 7.84%. It can be found that with the increase in the thickness of honeycombed steel web, the eccentrical compression bearing capacity of the specimens increases gradually. Figure 7(d) shows the load (N) versus the vertical displacement (Δ) relationships of the specimens with different space-depth ratio, and when the space-depth ratio increases from 0.15 to 1.4, the eccentrical compression capacity of the specimens increases from 12.42 × 10 3 kN to 13.12 × 10 3 kN, which raises by 5.64%, which indicates that with the increase in the space-depth ratio, the eccentrical compression capacity of specimens increases. e load (N) versus the vertical displacement (Δ) relationships of the specimens with different yield strength of the steel tube are illustrated in Figure 7(e), and when the yield strength of the steel tube increases from 235 MPa to 460 MPa, the eccentrical compression capacity of the specimens increases from 10.86 × 10 3 kN to 14.51 × 10 3 kN, which increases by 33.61%. It can be found that with the increase in the yield strength of the steel tube, the eccentrical compression bearing capacity of the specimens increases gradually. Figure 8 shows that with the increase in the eccentricity, the cubic compressive strength of concrete, the thickness of the steel tube flange, and diameter-depth ratio, the lateral deflection of mid-span sections of the specimens decreases gradually. e load-lateral deflection curves of the specimens with different parameters are illustrated in Figure 8. As the eccentricity of the specimens increases from 80 mm to 400 mm, the lateral deflection of mid-span sections decreases from 28.64 mm to 17.77 mm, which reduces by 37.94%, as shown in Figure 8(a). It can be found that the lateral deflection of mid-span sections of the specimens decreases gradually with the increase in eccentricity.

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can be found that with the increase in the cubic compressive strength of concrete, the lateral deflection of mid-span sections of the specimens decreases gradually. Figure 8(c) shows that as the thickness of the steel tube flange increases from 6 mm to 14 mm, the lateral deflection of mid-span sections decreases from 29.56 mm to 23.00 mm, which reduces by 22.19%. is indicates that with the increase in the thickness of the steel tube flange, the lateral deflection of mid-span decreases. Figure 8(d) shows that as the diameter-depth ratio increases from 0.1 to 0.75, the lateral deflection of mid-span sections decreases from 31.21 mm to 23.83 mm, which reduces by 28.32%. is indicates that with the increase in the diameter-depth ratio, the lateral deflection of mid-span sections of the specimens decreases. Figure 9 shows that with the increase in the slenderness ratio, the thickness of honeycombed steel web, space-depth ratio, and the yield strength of the steel tube, the lateral deflection of mid-span sections of specimens gradually increases. As the slenderness ratio of the specimens increases from 19.4 to 60.97, the lateral deflection of mid-span section increases from 21.94 mm to 53.87 mm, which raises by 145.53%, as shown in Figure 9(a). It can be found that the lateral deflection of mid-span sections of the specimens increases gradually with the increase in the slenderness ratio. Figure 9(b) illustrates the eccentrical load (N) versus lateral deflection (Δ) relationships of the specimens with different thickness of honeycombed steel web, in which as the thickness of honeycombed steel web increases from 8 mm to 16 mm, the lateral deflection of mid-span sections increases from 26.36 mm to 30.23 mm, which raises by 14.68%. It can be found that with the increase in the thickness of honeycombed steel web of the specimens, the lateral deflection of mid-span sections of the specimens decreases gradually.  Figure 9(c) shows that as the space-depth ratio of the specimens increases from 0.15 to 1.4, the lateral deflection of mid-span sections increases from 24.36 mm to 35.67 mm, which improves by 46.43%. It indicates that the lateral deflection of mid-span sections decreases with the increase in the space-depth ratio of the specimens. Figure 9(d) shows that as the yield strength of the steel tube increases from 235 MPa to 460 MPa, the lateral deflection of mid-span sections increases from 23.61 mm to 30.64 mm, which raises by 29.78%. is indicates that the lateral deflection of midspan sections increases with the increase in the yield strength of the steel tube of the specimens.

N/N u -M/M u Curves
. e numerical simulation results of the specimens reflect that with the increase in the slenderness ratio, the thickness of the steel tube flange, and diameter-depth ratio, the convexity of the N/N u -M/M u curves of the specimens gradually decreases, as illustrated in Figure 10. With the increase in the cubic compressive strength of concrete, the thickness of honeycombed steel web, space-depth ratio, and the yield strength of the steel tube, the convexity of the N/N u -M/M u curves of the specimens gradually increases, as shown in Figure 11, and the load transfer capacity of honeycomb steel web increases. Figure 10(a) illustrates that with the increase in the slenderness ratio of the specimens, the convexity of the N/ N u -M/M u curves of the specimens gradually decreases, and the inflection points of the curves become inconspicuously. e curves basically show a trend to be straight lines, and with the increase in the slenderness ratio of the specimens, the intersection points of the curves and the longitudinal axis close to the origin gradually, which indicates that with the increase in the slenderness ratio of the specimens, the   Advances in Civil Engineering deformation of the specimens becomes larger, and the second-order bending moment caused by the geometric deformation of the specimens increases, and the eccentric compression bearing capacity of the specimens decreases. It can be found from Figure 10(b) that with the increase in the thickness of the flange steel tube, the convexity of the N/N u -M/M u curve of the specimens gradually decreases. It can also be found that with the increase in the thickness of the flange steel tube, the constraint effect of the steel tube on the core concrete increases. Figure 10(c) shows that with the increase in the diameter-depth ratio, the convex degree of the N/N u -M/M u curve of the specimens decreases gradually. It can be seen that with the increase in the diameter-depth ratio, the inflection point of N/N u -M/M u curve moves left, which indicates that the load transfer capacity of honeycomb steel web decreases with the decrease in the diameter-depth ratio. Figure 11(a) shows that with the increase in the cubic compressive strength of concrete, the convexity of the N/N u -M/M u curves of the specimens gradually increases. It can be seen that with the increase in the cubic compressive strength of concrete of the specimens, the constraint effect of the steel tube on the core concrete decreases. It can be found from Figure 11(b) that with the increase in the thickness of the honeycomb steel web of the specimens, the convexity of the N/N u -M/M u curves of the specimens gradually increases. It can also be found that with the increase in the thickness of the honeycomb steel web, the ability of load transfer of the honeycomb steel web increases, and the inflection points of the N/N u -M/M u curves move upward.
As can be seen from Figure 11(c), the convexity of the N/ N u -M/M u curves of the specimens increases with the increase in the space-depth ratio, which shows that with the increase in the distance-to-height ratio, the capacity of load transfer of the honeycomb steel web increases. Figure 11(d) illustrates that with the increase in the yield strength of the steel tube, the convex degree of N/N u -M/M u curves of the specimens increases gradually, which indicates that with the increase in the yield strength of the steel tube, the constraint effect of the steel tube on concrete increases obviously.

Lateral Deflection Curves.
Five full-scale specimens are selected from 33 STHCCs as representative examples, and the representative specimens exhibit different eccentricity. e lateral (H)-deflection (Δ) curves of the five specimens subjected to eccentrical compression are shown in Figure 12. It is noteworthy that the H-Δ curves of the specimens are basically symmetrical distribution. e maximum deflection appears at the mid-span sections of the specimens, and the increase in the deflection is proportional to the increase in the eccentricity.

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When the load reaches 0.9N u , the deflection begins to rapidly increase, and eventually, the column destroys. e development regularity of the H-Δ curves of the STHCCs subjected to eccentrical compression is obtained, which is consistent with the development regularity of the ordinary square CFST columns under eccentrical compression [29].

Strain Distribution on Sections.
Taking STHCC-1, STHCC-2, STHCC-3, STHCC-4, and STHCC-5 as representative examples, the longitudinal strain distribution of the mid-span section of the specimens under eccentrical compression is computed, as shown in Figure 13. During the loading process, the longitudinal strain of the mid-span section conforms to the plane-section assumption. At the early stage of the loading, namely, the elastic working stage, the longitudinal strain of the mid-span section is in good agreement with the plane-section assumption, which shows that the steel tube coordinated with the core concrete [30,31].
When the load reaches 0.9 N u , the steel tube in the compression side yields firstly, and the obvious bulging appears on steel tube, simultaneously the concrete is crushed, which indicates that both cannot work in coordination with each other. It is also found that with the increase in the eccentricity, the neutral axis of the mid-span section moves to the loading point gradually. Figure 14 shows the load (N) versus strain (ε) relationships of point A and point E of specimen STHCC-1, and it can be seen from Figure 14 that at the initial stage of the loading, the strain and load of the tension and compression zone of STHCCs increase proportionally with the increase in the load. During the loading process, the longitudinal strain of the compression zone is greater than that of the tension side under the same load. When the load reaches about 95% of the ultimate load, the compression side of the steel tube yields firstly, and the mutual coordination between the steel tube and the core concrete is destroyed, eventually the overall specimen is bent and unstable. e stress cloud diagram of each part of specimen STHCC-1 is illustrated in Figure 15.

Eccentric Compression Bearing Capacity of Full-Scale STHCCs
e simplified calculation method on eccentrical compression bearing capacity for reduced-scale STHCCs has been proposed by Ji et al. [15], which can be expressed as (3). e specific meaning of variables is illustrated in reference [15].

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Equation (3) is adopted to calculate the eccentrical compression bearing capacity (N c c ) of 33 full-scale specimens, and the dispersion comparison between N c c and N a for 33 specimens is shown in Figure 16. As can be seen in Figure 16, the maximum error is 43.24%. It is noteworthy that the calculation formula of eccentrical compression bearing capacity obtained based on the reduced-scale model has certain limitations; thus, it is not suitable for calculating the eccentrical compression bearing capacity of full-scale composite columns. So the calculation formula of eccentrical compression bearing capacity of full-scale composite columns needs to be put forward. e equation of the N/N u -M/M u curves for CFST composite columns proposed by Han <u> [32,33]</u> can be expressed as follows: where a � 1 − 2η 0 , b � (1 − ξ 0 )/η 2 0 , c � 2(ξ 0 − 1)/η 0 , and the significance of physical variables can be found in references [32,33].
According to the unified theory deduced by Han [32], the axial compression capacity (N u ) on bearing and flexural bearing capacity (M u ) of CFST columns can be obtained, which are given by where f scy � (1.18 + 0.64ξ) × f ck , A sc � A s + A c , ξ � A s × f y /A c × f ck , c m � 1.04 + 0.48 ln(ξ + 0.1), and W scm � (2I/h). e significance of physical variables is shown in reference [32].
Considering the influence of the eccentricity, the slenderness ratio, the cubic compressive strength of concrete, the thickness of steel tube flange, the thickness of honeycombed steel web, diameter-depth ratio, space-depth, and the yield strength of the steel tube on the mechanical behavior of fullscale STHCCs, the bias stability coefficient (φ) [34] is subsequently introduced, and the influence of second-order bending moment [34] of the medium-long columns is considered. e related equation of N/N u -M/M u curves is summarized as follows: e effects of different parameters on φ are illustrated in Figure 17.
According to the (6), the eccentrical compression bearing capacity (N c ) for 33 STHCCs can be calculated as shown in Table 3. By comparison, it can be seen from Figure 18 that the maximum error between N c and N a is 7.89%, which shows that both are in good agreement and can meet the requirements in actual engineering.

Conclusions
e eccentrical compression behavior analysis of 33 fullscale STHCCs was studied. e conclusions can be drawn as follows.
Based on the nonlinear constitutive model of concrete and simplified constitutive model of steel, the load-vertical displacement curves and load-lateral deflection curves of 15 square CFST columns were obtained by ABAQUS software. By comparison with the existing test data, both were in good agreement, which could verify the rationality of the material constitutive model and FE modeling method. e development regularity of lateral deflection curves for full-scale STHCCs is consistent with that of lateral deflection curves for CFST columns, and the maximum deflection appears at the mid-span sections of the specimens. e stress distribution along the cross-sectional height of the mid-span sections for full-scale STHCCs subjected to eccentrical compression basically conforms to the planesection assumption. e influence of parameters on eccentrical compression bearing capacity and lateral deflection is systematically investigated. It can be concluded that with the increase in e, λ, and d/h w , the eccentrical compression bearing capacity of specimens decreases gradually, whereas the eccentrical compression bearing capacity of specimens increases significantly with the increase in f cuk , t 1 , t 2 , s/h w , and f y . It can be found that the lateral deflection of the mid-span section decreases gradually with the increase in e, f cuk , t 1 , and d/h w , whereas the lateral deflection of the mid-span section gradually increases as λ, t 2 , s/h w , and f y increase. e calculation formula on eccentrical compression bearing capacity for STHCCs is proposed by statistical regression.

Data Availability
e data used to support the findings of this study are included within the article.

Conflicts of Interest
e authors declare that they have no conflicts of interest.