Research Article  Open Access
Hong Chang, Wei Zhou, "Stiffness and Crack Behavior of Unbonded Posttensioned Concrete Beam Strengthened with Aluminum Alloy Plate", Advances in Civil Engineering, vol. 2020, Article ID 3824543, 13 pages, 2020. https://doi.org/10.1155/2020/3824543
Stiffness and Crack Behavior of Unbonded Posttensioned Concrete Beam Strengthened with Aluminum Alloy Plate
Abstract
Corrosion resistance of aluminum alloy plates externally bonded by magnesium phosphate cement provides the ability to strengthen inshore infrastructures in harsh environments subject to moisture and humidity. In this study, the aim is to study the stiffness and cracking behavior of concrete beams using this strengthening technique. Six damaged unbonded posttensioned concrete beams were repaired and strengthened and then subjected to monotonic load until failure. This technique improved the stiffness and limited the development of cracks. The formula of elasticplastic stiffness coefficient related to the comprehensive reinforcement index was established. An influence coefficient δ considering the effect of aluminum alloy plates and unbonded tendons was introduced, and the crack expansion coefficient under shortterm load was obtained by statistical analysis. Finally, some simplified methods were proposed to evaluate the stiffness and cracks of unbonded posttensioned concrete beams strengthened with aluminum alloy plates.
1. Introduction
Numerous studies have verified the mechanical properties of structures strengthened by thin steel plates and fiber reinforced polymer (FRP) sheets, and the research results have contributed to the development of specifications, codes, and standards. Meanwhile, these techniques have been used widely in various infrastructures [1–8]. However, the corrosion of steel in wet or humid conditions can decrease its strengthening effect. In addition, the brittle failure characteristics of FRP does not meet the ductile requirements of concrete structures. As a strengthening material, there are two advantages of aluminum alloy (AA) compared to steel and FRP: (1) it has a similar tensile strength to steel, and lower density and (2) it has a similar corrosion resistance to FRP, and higher ductility. In addition, epoxy used as an adhesive for structural strengthening behaves poorly under high temperature and aging, and has a pungent odor. Magnesium phosphate cement (MPC) has the advantages of high strength, low shrinkage, high temperature resistance, aging resistance, and nontoxicity, and therefore has the potential to replace epoxy as the adhesive for structural strengthening in harsh environments [9, 10].
Previous studies [11–14] have shown experimentally that the technique of strengthening with AA plates can effectively improve the flexural capacity of reinforced concrete (RC) beams, with better ductility than that of beams strengthened with FRP. The RC beams strengthened by this technique have the behavior of debonding under the loading point, which is similar to the behavior shown by FRP sheet and steel plate and causes the premature failure of strengthened beams. The strengthening technique of nearsurface mounting with AA plates and external bonding using AA plates with anchoring can effectively avoid early failure of strengthened beams caused by debonding of AA plates. The formula of ACI 440.2R08 is found to be feasible to predict the debonding strain of the beams strengthened by AA plates. Epoxy was used as the adhesive for AA plates in most previous studies. Researchers have applied MPC to the interface between AA plates and concrete, studied the behavior of the interface through bilateral shear tests, and proposed the constitutive model of the bondslip relationship [15]. The feasibility of using MPC as the adhesive bonding AA plates to strengthen unbonded posttensioned concrete (UPC) beams has been proved [16]. The ductility of the strengthening beam decreased while the flexural capacity was effectively improved. Studies on stiffness and cracking of UPC beams strengthened by AA plates bonded with MPC have not yet been carried out.
In this study, an investigation was carried out on the stiffness and cracking of UPC beams strengthened with AA plates bonded by MPC. Six damaged UPC beams were repaired and strengthened, and then loaded to failure under a monotonic load, and attention was specifically paid to the deflection and cracks of the beams. Finally, a calculation method of stiffness and cracking of UPC beams strengthened with AA plates has been proposed based on experimental results and available theory.
2. Specimens and Methods
2.1. Specimens
A total of six damaged UPC beams were repaired and strengthened. Figure 1 shows the dimensions, reinforcement details, crosssection details, and unbonded prestressed details of the specimens. Each beam has a length of 6000 mm and different reinforcement ratios. The properties of specimens are shown in Table 1.
(a)
(b)

The reinforcement index of the nonprestressed reinforcements β_{s} = f_{y}A_{s}/f_{c}bh_{p}, that of the unbonded tendons β_{p} = σ_{pe}A_{p}/f_{c}bh_{p}, that of the AA plate β_{a} = σ_{a}A_{a}/f_{c}bh, that of the compression reinforcement β_{s}′ = f_{y}′A_{s}′/f_{c}bh_{p}, and the compositive reinforcement index β_{0} = β_{s} + β_{p} + β_{a−}β_{s}′, where b is the width of the UPC beams; h_{s}, h_{p}, and h_{a} are the distance from the top face to the centroid of the nonprestressed reinforcement, unbonded tendons, and AA plate, respectively. f_{y}, σ_{pe}, σ_{a}, and f_{y}′ are the yield stress of nonprestressed reinforcement, unbonded tendons, AA plate, and compression reinforcement, respectively.
All six UPC beams were damaged by static loads, followed by the crushing of the concrete in the compression zone. All the damaged beams exhibited relatively small residual deformation, and most of the tensile cracks were closed. The reinforcement yielded before the concrete in the compression zone crushing. The initial damage of each damaged UPC beam is shown in Table 2.

The diameter of the stirrup of the specimens was 8 mm, which was distributed in the range of 2000 mm at the end of the beams with a spacing of 100 mm (see Figure 1). The stainlesssteel bolts with a diameter of 10 mm were anchored into the hole with a depth of 50 mm at the bottom of the beams with MPC. The uses of the stainlesssteel bolts are as follows: (1) to bear the interfacial shear force when the bonding fails; (2) to avoid the debonding of the AA plates before the failure of strengthened beams; (3) to apply uniform pressure to the AA plates in the setting process of MPC to improve the adhesion effect. Considering the above factors, it was determined that the stainlesssteel bolts would be staggered with a spacing of 330 mm (see Figure 2).
2.2. Properties of Materials
Concrete with grade 40 was used to cast the beams. P.O 42.5 Portland cement and class F fly ash were used as binders, with a waterbinder ratio (/b) of 0.3. Sand particles in zone II were used as the fine aggregate, and crushed rocks were used as coarse aggregate. The axially compressive strength of the concrete was 45 MPa. The elastic modulus of the concrete E_{c} was 33600 MPa.
Steel strands of grade 1860 with a diameter of 17.8 mm were used as unbonded tendons. Their tensile strength was 1915 MPa, and nominal yield strength was 1732 MPa. The mechanical properties of nonprestressed reinforcements are shown in Table 3.

A unidirectional tensile test of 5083 AA plates was carried out on a universal electronic test machine (see Figure 3), which showed that its yielding strength was 112 MPa, ultimate strength was 210 MPa, elastic modulus E_{a} was 278000 MPa, and ultimate elongation was 27%.
MPC is composed of ammonium dihydrogen phosphate or potassium dihydrogen phosphate, magnesium oxide, and a setting retarder. Borax was used as a retarder agent in this experiment, and the mix ratio of MPC by weight was ammonium dihydrogen phosphate (NH_{4}H_{2}PO_{4}): borax (Na_{2}B_{4}O_{7} · 10H_{2}O): magnesium oxide (MgO): water = 26 : 4:51 : 19. The compressive strength and flexural strength of the MPC were 23.5 MPa and 7.5 MPa, respectively.
2.3. Experimental Designs
Twopoint loads were applied at the onethird span points of the beam (see Figure 4). Three displacement sensors were set under the loading points and the midspan of the beam, two sensors were located at the end of the AA plate to measure the relative slip between the AA plate and the beam, and another two were set above the supports to measure the beam end movement. The AL beams were loaded with 5 kN for each level, and the AS beams with 3 kN for each level.
2.4. Failure Modes
Among the six specimens, the failure mode of SS3 was the sudden fracture failure, and the failure of the other five beams can be attributed to concrete crushing in the compression zone. The details are as follows.
3. Stiffness Analysis
3.1. Relationship between Load and Deflection
The typical curve of loaddeflection of prestressed concrete beams should have obvious turning at the points of cracking of beams and yielding of nonprestressed reinforcements. In this study, the test beams have been damaged and repaired, which has a certain impact on the stiffness of strengthened beams. As a result, the stiffness mutation of strengthened beams was not obvious, as shown in Figure 5. The attached figures show the characteristics of a trilinear model with the inflection points of the crack load, yield load, and ultimate load of strengthened beams. It can be observed from Figure 5 that the curves still have similar characteristics to those of the prestressed concrete beams.
(a)
(b)
(c)
(d)
(e)
(f)
The three dotted lines were divided into three stages, with the slope of each segment being the stiffness of the corresponding stage.
Stage I is the stage before the concrete cracks. The beam behaves mainly elastically. The relationship between stress and strain is basically linear. This stage continued until the tensile stresses exceeded the tensile strength of concrete.
Stage II is the serviceability stage that occurs after the concrete has been cracked and nonprestressed reinforcements take up almost all the tension force, but the nonprestressed reinforcements have not yet yielded. The neutral axis shifts upward with the increase of the applied loads.
Stage III starts with the yielding of nonprestressed reinforcements and ends with the failure of the beam. In this stage, the stiffness of the beam is weakened further. The loaddeflection relationship becomes clearly nonlinear. Finally, the excessive developing of cracks and the crushing of concrete in the compression zone lead to the ultimate collapse of the beam.
Figure 5 shows that the stiffness changes of the SL1 and SS1 beams with the lowest reinforcement ratio are obvious at the crack load, while those of other beams are not obvious. The behavior at the yield load is opposite to that at the crack load; the stiffness of the SL1 and SS1 beams does not change significantly at the yield load, while the stiffness of other beams changes significantly at the yield load. It can be concluded that (1) the influence of cracking on the stiffness is inversely proportional to the reinforcement ratio and (2) the influence of the yielding of nonprestressed reinforcement on the stiffness is proportional to the reinforcement ratio.
Figure 6 shows the failure modes of the specimens.
(a)
(b)
(c)
(d)
(e)
(f)
3.2. Stiffness Calculation
A formula for calculating the deflection of homogeneous elastic materials is proposed in [17], , but the concrete is a heterogeneous and inelastic material, so the bending stiffness of the interface changes during bending. The bending stiffness not only decreases with the increase of load but also decreases with the increase of load duration, so the reduction coefficient, namely, the elasticplastic stiffness coefficient, should be considered. According to the empirical values used in the Chinese design standards, the elasticplastic stiffness coefficient of concrete beams before cracking is 0.85, and the elasticplastic stiffness coefficient after cracking β′ needs further research.
According to the bilinear stiffness model, the bending momentdeflection curve of prestressed concrete beams can be regarded as consisting of two straight sections OA and AB. With the cracking point as the turning point, the deflection under the cracking moment M_{cr} is f_{cr}, and the deflection under the serviceability moment is f_{s}, as shown in Figure 7.
According to Figure 5, .
The elasticplastic stiffness coefficient under the increment of bending moment (M_{s} − M_{cr}) is then obtained aswhere a is the coefficient of load and support conditions, which according to the material mechanics, in this case, is 0.106.
In order to study the elasticplastic stiffness coefficient β′ after cracking, it is necessary to analyze the bending moment increment, and M_{s} is calculated as 1.67M_{cr}. It was found by calculation that when the M_{s} of the SL1 beam was 150 kN, the nonprestressed reinforcements have yielded, so no research was conducted on the SL1 beam. According to the experimental data of the other five strengthened beams, the elasticplastic stiffness coefficient was as calculated in Table 4.

By analysis of the experimental data, it was found that there was an approximate linear relationship between 1/β′ and 1/β_{0}, and the fitting equation is as equation (2) with a correlation coefficient of 0.9588. Figure 8 shows the relationship between experimental data and the fit line:
Thus,
The stiffness of a UPC beam changes during bending; therefore, in order to accurately calculate the deformation of the beam under shortterm load, an appropriate average stiffness B_{s} is proposed as the shortterm stiffness. Thus, on the basis of , the shortterm stiffness of UPC beams strengthened by AA plates can be expressed as
3.3. Prediction and Analysis of Deflection
A UPC beam can be regarded as equivalent to an RC beam with a pair of prepressure in the anchorage position, which still show the characteristics of an RC beam after cracking. Therefore, the stiffness of UPC beams strengthened with AA plates can be measured using the same research method as the RC beams.
The stiffness under shortterm load of the strengthened beam was constant before cracking, so the stage before cracking has not been investigated, and the deflection under shortterm load of five strengthened beams, apart from SL1, was analyzed.
The value of B_{s} is substituted into equation (4) to calculate the deflection of the strengthened beam after cracking, and the calculation results are shown in Table 5. Although most of the deflection of UPC beams in the initial damage was restored by the prestress, there were still some residual deflection that was not restored, which has been taken into account.

The calculation errors by the method proposed in this study were all within 10%, so the calculation method is applicable to the stiffness calculation of UPC beams strengthened by AA plates.
4. Crack Analysis
4.1. Mean Crack Spacing
The crack development mechanism of UPC beams is similar to that of RC beams. When the concrete in the tensile zone cracks, the concrete is no longer in tension, but the nonprestressed reinforcement continues to undergo tension. Due to the difference in the elastic modulus of concrete and steel, the tension causes a relative slip between the nonprestressed reinforcements and the concrete bonded with them, which causes the development of cracking. During this process, there is no bond force between the unbonded prestressed tendons and concrete, and the tensile stress of concrete in the tensile zone is offset by the prestress of unbonded prestressed tendons in the initial period of loading. Prestress can delay the occurrence of cracking in the concrete, but it cannot control the distribution of cracks, which are mainly controlled by the relationship of bondslip between the nonprestressed reinforcement and the concrete.
The experimental results show that the cracks in the tensile concrete of the strengthened beams are all the same as in the initial damage, and no new cracks appeared. The experimental data also show that there is a regular relationship between the mean crack spacing l_{cr} and d_{eq}/ρ_{s} and t_{a}/ρ_{a}, with the regression equation as follows:
The correlation coefficient of the above equation is 0.9538, where d_{eq} is the equivalent diameter of the reinforcement, t_{a} is the thickness of the AA plate, ρ_{s} and ρ_{a} are the reinforcement ratios of the nonprestressed reinforcement and AA plate, respectively.
Table 6 shows the results calculated by equation (5) and the experimental results. The calculated errors are all less than 5%, indicating that it is suitable for calculating the mean crack spacing of UPC beams strengthened by AA plate.

4.2. Mean Crack Width
4.2.1. Stress Increment of Unbonded Prestressed Tendons in Serviceability Stage
In the initial loading, the stress in the unbonded prestressed tendons grew slowly. After the concrete in the tension zone cracked, the stress in the unbonded prestressed tendons grew quickly. The cracks then gradually developed, the stiffness gradually declined, and the deformation increased more quickly. Due to the different reinforcement ratio, initial prestress, and other parameters of each strengthened beam, the stress increment of the unbonded prestressed tendons could not be compared directly. In order to have a unified comparison standard for the strengthened beams, the relative values of the stress increment and prestress of each strengthened beam were analyzed. Based on the experimental results, it was found that there was a linear relationship between Δσ_{p}/Δσ_{py} and (M_{k} − M_{cr})/(M_{y} − M_{cr}) in the serviceability stage, described as follows:
The correlation coefficient of the fit line was 0.94, where Δσ_{p} is the stress increment of unbonded tendons in the serviceability stage, Δσ_{py} is the stress increment of the unbonded tendons when the nonprestressed reinforcements were yielding, M_{k} is the bending moment in the serviceability stage, and M_{y} is the bending moment when the nonprestressed reinforcements were yielding. The relationship between the fit line and the experimental data of each test beam is shown in Figure 9.
4.2.2. Stress Increment of Unbonded Tendons When the NonPrestressed Reinforcement Is Yielding
In order to calculate Δσ_{p} using equation (6), the equation governing Δσ_{py} needs to be established.
Analysis of the experimental data shows that Δσ_{py} has a regular relationship with β_{0} and β_{s}, with the fitting equation as follows:
The fitting curve has a correlation coefficient of 0.9309. The relationship between experimental data and fit line is shown in Figure 10.
The results of Δσ_{py} calculated by equation (7) and the experimental data are shown in Table 7. It can be seen that the error was within 10% except for the SS2 beam with large dispersion. Therefore, equation (7) is applicable to the calculation of the stress increment of unbonded tendons when the nonprestressed reinforcement is yielding.

Equation (6) can be translated into
When equation (8) is substituted into equation (7), the formula for Δσ_{py} can be obtained as follows:
4.2.3. Bending Moment in Serviceability Stage
The serviceability stage of a UPC beam usually refers to the period between beam cracking and yielding of nonprestressed reinforcement. The cracking moment can be expressed aswhere W_{0} is the bending modulus of the transformed section, σ_{py} is the prestress of the tensile edge of the concrete while deducting all losses, and f_{tk} is the characteristic value of axial compressive strength.
The distribution of stress and strain of the cross section when the nonprestressed reinforcement was yielding is shown in Figure 11.
(a)
(b)
(c)
From Figure 11, the tensile force is equal to the resultant compression force:
In equation (11),
The experimental data show that the yielding in the nonprestressed reinforcement was earlier than that in the AA plate. Therefore, when the nonprestressed reinforcement was yielding, the distribution of stress and strain in the cross section conforms to the planesection assumption. So,
Equation (14) can be translated as
According to equations (11), (12), (13), and (15), the depth of the compression zone when the nonprestressed reinforcement was yielding can be obtained, and the yielding moment can be expressed as
4.2.4. Mean Crack Width
The distribution of stress and strain of the cracking section in the serviceability stage is shown in Figure 12.
(a)
(b)
For equilibrium, the following equation can be established:where N_{pe} is the prepressure compression, η_{s}h_{0}, η_{p}h_{p}, and η_{a}h are, respectively, the internal force arms of the nonprestressed reinforcement, unbonded tendons, and AA plate which undergoes the bending moment.
In the process of crack development of UPC beams, the contribution of unbonded prestressed tendons to the crack resistance of the UPC beam is less than that of the same quantity of bonded prestressed tendons. Therefore, a reduction factor α for the unbonded tendons has been introduced in equation (17), which is the ratio of the stress increment of unbonded prestressed tendons to that of nonprestressed reinforcement at the same location with service load. According to the existing research [18], the recommended value of α is 0.23.
According to the planesection assumption, the stress in nonprestressed reinforcement in the serviceability stage is as follows:
This can be translated to
In the above, z is the distance from the point of the resultant force of nonprestressed reinforcement and unbonded tendons to the centre of compression of the concrete, which can be calculated by the following equations:where e is the distance between the action point of axial pressure and that of the resultant force of the nonprestressed reinforcement and e_{p} is the distance between the action point of prepressure and that of the resultant force of the unbonded tendons, nonprestressed reinforcement, and AA plate.
According to the development mechanism of cracks in reinforced concrete beams, the mean crack width of the beams is approximately the difference between the elongation of nonprestressed reinforcement and the elongation of concrete at the corresponding position within the crack spacing. The formula for the mean crack width of a UPC beam is as follows:where ψ is the coefficient of uniformity of nonprestressed reinforcement, which can be calculated according to the following formula:where ρ_{te} is the reinforcement ratio of nonprestressed reinforcement calculated according to the effective tensile area of concrete and considering the effect of the AA plate, and ρ_{te} = (A_{s} + E_{a}A_{a}/E_{s})/A_{te}, where A_{te} is the effective tensile area of concrete, and A_{te} = 0.5bh, f_{tk} is the characteristic value of concrete axial compressive strength.
4.3. Maximum Crack Width
Previous studies showed that the crack width of the RC beams has a large dispersion, and the reasonable maximum crack width should be determined by statistical analysis. According to this study, the distribution of the ith crack width to the mean crack width under shortterm loading, it was found that the value of was approximately a normal distribution, as shown in Figure 13.
The fitting equation of the normal distribution curve is as follows:with a correlation coefficient of 0.9661.
The maximum crack width is determined by the guarantee rate of 95%, and the characteristic value corresponding to is the crack expansion coefficient under shortterm loading τ_{s}:
Thus, the equation for calculating the maximum crack width under the shortterm load is as follows:
Even if the load remains unchanged under a longterm load, due to shrinkage, creep, and slippage of the concrete in the tension zone, the concrete in tension between the cracks will continuously break away, and the strain of the nonprestressed reinforcement near the cracks will gradually increase. The crack width of the beam will thus increase over time. Therefore, the effect of longterm loading should be considered in the calculation of cracks, and the expansion coefficient t_{l} should be introduced. According to previous studies, t_{l} = 1.5 [19]. Thus, the calculation equation for the maximum crack width of UPC beams strengthened with AA plates under longterm loading is as follows:
5. Conclusion
(1)The technique of strengthening UPC beams with AA plates can improve stiffness and limit the development of cracks.(2)The relationship of the loaddeformation curve of damaged beams strengthened with AA plates is different from that of typical reinforced concrete beams, i.e., the characteristic trilinear model with cracking and yielding as inflection points of the strengthened beams was less obvious than that of undamaged reinforced concrete beams.(3)Based on the double broken line model, an equation for the elasticplastic stiffness coefficient in the serviceability stage with integrated reinforcement index β_{0} as parameter was proposed, and a calculation method for the stiffness of a UPC beam strengthened with AA plates was proposed.(4)The relative relationship between average crack spacing l_{cr}, d_{eq}/ρ_{s}, and t_{a}/ρ_{a} was analyzed, and a calculation method of mean crack spacing for UPC beams strengthened with AA plates was proposed by regression.(5)Based on the analysis of the stress increment of unbonded prestressed tendons in the serviceability stage, a calculation method was proposed. An influence coefficient considering the effect of unbonded prestressed tendons and AA plates was introduced, and a calculation method for the crack width in UPC beams strengthened with AA plates was proposed.
The behavior of concrete structures strengthened with aluminum alloy plate in corrosive environments should be studied in future research.
Data Availability
The raw/processed data required to reproduce these findings cannot be shared at this time as the data also form part of an ongoing study.
Disclosure
The funders had no role in the design of the study; in the collection, analyses, or interpretation of data; in the writing of the manuscript; or in the decision to publish the results.
Conflicts of Interest
The authors declare no conflicts of interest.
Acknowledgments
The authors are grateful to the members of their research group in Civil of HIT, and they are appreciated for their effort in the investigation. This research has been supported by the National Natural Science Foundation of China (NSFC) under grant no. 51778186.
References
 M. C. Sundarraja and S. Rajamohan, “Strengthening of RC beams in shear using GFRP inclined strips—an experimental study,” Construction and Building Materials, vol. 23, no. 2, pp. 856–864, 2009. View at: Publisher Site  Google Scholar
 I. F. Kara, A. F. Ashour, and M. A. Köroğlu, “Flexural behavior of hybrid FRP/steel reinforced concrete beams,” Composite Structures, vol. 129, pp. 111–121, 2015. View at: Publisher Site  Google Scholar
 B. H. Oh, J. Y. Cho, and D. G. Park, “Static and fatigue behavior of reinforced concrete beams strengthened with steel plates for flexure,” Journal of Structural Engineering, vol. 129, no. 4, pp. 527–535, 2003. View at: Publisher Site  Google Scholar
 L. Huang, B. Yan, L. Yan, Q. Xu, H. Tan, and B. Kasal, “Reinforced concrete beams strengthened with externally bonded natural flax FRP plates,” Composites Part B: Engineering, vol. 91, pp. 569–578, 2016. View at: Publisher Site  Google Scholar
 S. Aykac, I. Kalkan, B. Aykac, S. Karahan, and S. Kayar, “Strengthening and repair of reinforced concrete beams using external steel plates,” Journal of Structural Engineering, vol. 139, no. 6, pp. 929–939, 2013. View at: Publisher Site  Google Scholar
 S. S. Choobbor, R. A. Hawileh, A. A. AbuObeidah, and J. Abdalla, “Performance of hybrid carbon and basalt FRP sheets in strengthening concrete beams in flexure,” Composite Structures, vol. 227, Article ID 111337, 2019. View at: Publisher Site  Google Scholar
 O. R. Abudodeh, J. A. Abdalla, and R. A. Hawileh, “Prediction of shear strength and behavior of RC beams strengthened with externally bonded FRP sheets using machine learning techniques,” Composite Structures, vol. 234, Article ID 111698, 2020. View at: Publisher Site  Google Scholar
 M. Z. Naser, R. A. Hawileh, and J. A. Abdalla, “Fiberreinforced polymer composites in strengthening reinforced concrete structures: a critical review,” Engineering Structures, vol. 198, Article ID 109542, 2019. View at: Publisher Site  Google Scholar
 A.J. Wang, N. Song, X.J. Fan et al., “Characterization of magnesium phosphate cement fabricated using prereacted magnesium oxide,” Journal of Alloys and Compounds, vol. 696, pp. 560–565, 2017. View at: Publisher Site  Google Scholar
 H. Ma and B. Xu, “Potential to design magnesium potassium phosphate cement paste based on an optimal magnesiatophosphate ratio,” Materials & Design, vol. 118, pp. 81–88, 2017. View at: Publisher Site  Google Scholar
 J. H. Zhu, L. L. Wei, M. C. Zhu, W. W. Li, and F. Xing, “Experimental study of bond behavior on aluminum alloy platetoconcrete interface,” Applied Mechanics and Materials, vol. 501–504, pp. 805–810, 2014. View at: Publisher Site  Google Scholar
 J. H. Zhu, M. C. Zhu, L. L. Wei, W. W. Li, and F. Xing, “Bond behavior of aluminum laminates in NSM technique,” Applied Mechanics and Materials, vol. 501–504, pp. 1053–1060, 2014. View at: Publisher Site  Google Scholar
 J. H. Zhu, L. L. Wei, W. T. Wu, F. Xing, and R. Feng, “Experimental study of concrete strengthened by stiffened aluminum plate,” Applied Mechanics and Materials, vol. 584–586, pp. 997–1000, 2014. View at: Publisher Site  Google Scholar
 H. A. Rasheed, J. Abdalla, R. Hawileh, and A. K. AlTamimi, “Flexural behavior of reinforced concrete beams strengthened with externally bonded Aluminum Alloy plates,” Engineering Structures, vol. 147, pp. 473–485, 2017. View at: Publisher Site  Google Scholar
 H. Chang and W. Zhou, “Flexural behaviour of unbonded posttensioned concrete beam strengthened with aluminium alloy plates,” Mathematical Problems in Engineering, vol. 2020, Article ID 6535609, 13 pages, 2020. View at: Publisher Site  Google Scholar
 H. Chang and W. Zhou, “Experiment on bond behavior of aluminum alloy bonded to concrete by inorganic adhesive,” Journal of Harbin Institute of Technology, vol. 51, no. 6, pp. 58–63, 2019. View at: Publisher Site  Google Scholar
 F. P. Beer, E. Russell Johnston, J. T. DeWolf, and D. F. Mazurek, Mechanics of Materials, China Machine Press, Beijing, China, 6th edition, 2013.
 W. Z. Zheng and H. Y. Xie, “Calculation methods of stiffness and crack width of UPC beam in accordance with bonded pc beam,” Journal of Building Structures, vol. 3, pp. 65–69, 2005. View at: Publisher Site  Google Scholar
 Ministry of Construction, Code for Design of Concrete Structures. GB 500102010, Ministry of Construction, Beijing, China, 2010.
Copyright
Copyright © 2020 Hong Chang and Wei Zhou. 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.