CC BY
0Polymers 2014, 6, 1366-1380; doi:10.3390/polym6051366
OPEN ACCESS
polymers
ISSN 2073-4360
www.mdpi.com/journal/polymers
Article
Effect of Shear Resistance on Flexural Debonding Load-Carrying Capacity of RC Beams Strengthened with Externally Bonded FRP Composites
Guibing Li '*, Aihui Zhang and Weiliang Jin
1 Department of Management Science and Engineering, Shandong Institute of Business and Technology, Yantai 264005, China
2 College of Civil Engineering & Architecture, Zhejiang University, Hangzhou 310058, China; E-Mail: zah@zju.edu.cn
3 Ningbo Institute of Technology, Zhejiang University, Ningbo 315100, China; E-Mail: Jinwl@zju.edu.cn
* Author to whom correspondence should be addressed;
E-Mail: liguibing@zju.edu.cn or leegb@sina.com; Tel.: +86-535-690-3575.
Received: 8 February 2014; in revised form: 29 April 2014 /Accepted: 4 May 2014 / Published: 13 May 2014
Abstract: Debonding failure is the main failure mode in flexurally strengthened reinforced concrete beams by externally bonded or near surface mounted fibre reinforced polymer (FRP) composites. It is believed that FRP debonding will be initiated if the shear stress on the concrete-FRP interface reaches the tensile strength of concrete. However, it was found through experimental and analytical studies that the debonding mechanism of FRP composites has the potential of shear failure in combination with debonding failure. Moreover, the shear failure probably influences the debonding failure. Presently, there are very little experimental and analytical studies to investigate the influence of shear resistance of reinforced concrete (RC) beam on FRP debonding failure. The current study investigates and analyzes the effect of shear resistance on FRP debonding failure based on test results. The analytical results show that the shear resistance of RC beam has a great effect on flexural debonding load-carrying capacity of FRP-strengthened RC beam. The influence of shear resistance on flexural debonding load-carrying capacity must be fully considered in flexural strengthening design of RC beams.
Keywords: reinforced concrete (RC) beam; carbon fiber reinforced polymer (CFRP)-strengthened; shear resistance; flexural debonding load-carrying capacity
1. Introduction
Debonding failure is the dominant failure mode in flexurally fiber reinforced polymer (FRP)-strengthened reinforced concrete (RC) beams by externally bonded or near surface mounted FRP composites. According to initial debonding position, debonding failure is classified into two types: end debonding and intermediate crack induced debonding (IC debonding). The intermediate cracks are mainly referred to as the critical flexural crack and flexure-shear crack [1]. End debonding failure can be prevented by ensuring effective bond length of FRP composites [2-6]. Furthermore, some fracture mechanics analyses confirmed that the extension of bond length beyond effective bond length has no effect on debonding capacity [7-10]. However, IC debonding failure cannot be easily overcome. Kim and Harris conducted a statistical analysis of failure modes on 230 FRP-strengthened RC beams by externally bonded FRP composites. The statistical results show that about 81.7% of the beams failed by FRP debonding; 9.6% of the beams failed by cover delamination [11]. FRP debonding together with concrete cover delamination are the main failure mode in flexurally FRP-strengthened RC beams. Over the past decade, considerable experimental and analytical studies have been carried out to investigate IC debonding failure [11-22]. The experimental variables against IC debonding failure include concrete strength, amount of FRP reinforcement, effective bond length, surface preparation of the concrete substrate, sustained load level (or damage level) on RC beam at bonding FRP composites, allowable tensile strain of FRP reinforcement and anchorage methods for FRP composites, etc.
To prevent debonding failure, numerous debonding criteria and effective bond length models have been proposed. These criteria and models can be classified into three distinct categories: allowable tensile strain in FRP composites based on the single-shear test on FRP-to-concrete joints [11,14,23-29], shear stress limitation on the FRP-concrete interface [30-33], and fracture mechanics based models [7-10,24,27,34,35].
With extensive experimental investigations having been conducted on the flexural behavior of RC beams with externally bonded FRP composites, a noteworthy problem regarding the debonding mechanisms had emerged that the debonding failure is the potential of shear failure in combination with debonding failure [36]. It was found in experimental investigation that the width of critical shear-flexure crack and the relative vertical displacement between the two halves of this crack that are related with the shear resistance of RC beam have effect on debonding failure of RC beams with externally bonded FRP composites [37-43]. However, there are very limited experimental and analytical studies to examine the influences of shear resistance of RC beam on debonding failure.
It appears that ensuring adequate shear resistance of the beam must be considered as the priority in flexural strengthening design. The objective of this study is to investigate this issue according to corresponding test results.
2. Existing Experimental Findings and Conclusions in the Literature
Garden et al. [37,38] carried out four points bending and cantilever loading tests to investigate the influence of shear span/depth ratio, FRP plate anchorage length, and additional plate end anchorage on ultimate capacities and failure modes of reinforced concrete beams externally strengthened with bonded FRP plates. The main failure mode was FRP debonding with partial cover separation. The debonding characteristic is that a tributary crack formed adjacent to the main crack, forming a triangular shape bounded by the main crack, the tributary crack and the soffit of the beam. Opening-up of the main crack at beam soffit level was associated with the formation of relative vertical displacement at the tip of the tributary crack between the two halves of the main crack. The relative displacement became more pronounced with increasing applied load on the beam. Plate debonding propagated away from the tip of tributary crack to FRP plate end.
Rabinovitch and Frodtig [39] experimentally investigated the debonding failure triggered by edge effects, the stress concentration arisen near the edge of FRP strip, and the means for prevention of debonding failure. The debonding failure was triggered by the formation of critical flexure-shear crack at the shear span. The flexure-shear crack was usually associated with discontinuity in the vertical deflections of beam sections left and right of the cracked section. The interfacial delamination was initiated at the tip of the flexure-shear crack and propagated toward the support.
Pham and Al-Mahaidi [40,41] carried out a testing program including 18 rectangular reinforced concrete beams to investigate their failure mechanisms. The test varaibles are the carbon fiber reinforced polymer (CFRP) bond length, the number of plies, the area of tension reinforcement, the amount of shear reinforcement, and the concrete cover. The main failure mode was FRP laminates debonding. The critical flexural-shear crack under the loading point initiated the delamination of FRP laminates from the concrete substrate as the result of the high tensile force in FRP laminates and the vertical movement near its tip. More rotation was observed, the left part of the beam in the shear span tried to rotate to the right but it was held back by the FRP laminates. This leaded to the appearance of debonding cracks near the tip.
Yang et al. [43] employed four-point bending on flexurally strengthened RC beams externally bonded CFRP sheets with different bond length and U strip anchor at the laminate end to investigate the flexural debonding load-carrying capacity and debonding modes. It was found that the critical shear-flexure crack near the loading point was opening up gradually with the increasing of applied load. When the applied load reached a certain level, debonding occurred at the tip of the critical crack. Moreover, the shear span of the beam rotated significantly round the critical section. CFRP laminates debonded and propagated towards the direction of decreasing moment.
To verify the influence of relative vertical displacement on FRP debonding failure, Yao et al. [44] and Pan et al. [45,46] carried out experimental studies to investigate the effect of relative vertical displacement on FRP debonding. Their test results showed that the relative vertical displacement has great effect on the load-carrying capacity of the test members.
All the above experimental results have the same finding that the debonding of FRP laminates initiated at or near the tip of the main crack (or the tributary crack) and a relative vertical displacement developed between the left and right section of the main crack. For debonding induced by a flexural crack, the crack widening is the driving force for the debonding. The widening of the crack is also
more important than the relative vertical displacement in the debonding failure induced by critical flexural-shear crack [47].
3. Experimental Programs
Zhang et al. [42] tested 16 RC beams flexural-strengthened with externally bonded FRP sheets under four points bending, these beams were divided into four series A1, A2, B1, and B2, respectively. The test variables include the sustained load level on RC beams at bonding FRP sheets, the amount of FRP sheets, and the amount of tension rebar, respectively. The main objective of this experimental study was to investigate the effect of sustained load level on the flexural performance of FRP-strengthened RC beams.
Li et al. [48] carried out experimental study by three-point bending 6 FRP-strengthened RC beams which divided into two series C1 and C2. Test variables are sustained load level on RC beams at bonding FRP sheets, amount of FRP sheets, and anchorage of FRP sheets at beam-column joint. The main purpose of the test was to investigate the flexural performance of beam section at negative moment region strengthened by bonding FRP sheets. The details of all tested specimen by Zhang et al. [42] and Li et al. [48] are listed in Table 1; Material properties are listed in Table 2.
The soffit of the beam to bond CFRP laminate was firstly ground and cleaned to ensure good bonding. Then loads were applied on the test beams to the desired preload level. With maintaining the load, on the clean and flat surface, primer, epoxy, and CFRP laminates were applied in sequence. After the epoxy resin had been completely cured, additional loads were applied up to the failure of the beam.
In addition to the main objectives in the experimental studies by Zhang et al. [42] and Li et al. [48], the debonding process and characteristics were also investigated as one of the main goals. For the convenience of bonding FRP sheets and ensuring bonding quality, reverse loading was used in the experimental tests, as shown in Figure 1.
Figure 1. Test-setup of A2 and B2 series.
dial indicators
speciman
- guages
distribution beam
Load Cell
oil jack
Table 1. Dimensions of specimen and reinforcement materials.
Series
Dimensions of Beam
n x dia.
n x tf
Stirrup
dia.-s *
A10, A13, A16, A18 750
B10, B13, B16, B18 750
A20, A23, A26, A28 750
B20, B23, B26, B28 750
D1 600
D2 600
D3 600
D4 600
Stirrup(dia.-s) Rebar(n*dia.)
500 500 500 500 600 600 600
250 250 250 250 200 200 200 200
120 120 120 120 100 100 100 100
20 20 20 20 20 20 20 20
n*dia.
2000 2000 2000 2000 2000 2000 2000 2000
1800 1800 1800 1800 1620 1620 1620 1620
2 4 12 2 i 16 2 i 12 2 i 16 2 i 12 2 i 12 2 4 12 2 i 12 to 16
1 x 0.11
1 x 0.11
2 x 0.11 2 x 0.11
1 x 0.11
2 x 0.11 1 x 0.11
1 x 0.11
120 120 120 120 80 80 30 + 30 80
48-100 4 8-75 48-100 4 8-75 i 6-90 i 6-90 4 6-90 i 6-90
U50j_ 1250 400 1250 150 1 - 1 2 - 2
C10 1250 - 400 300 40 3200 1100 4 4 16 1 x 0.111 300 * 8-100
C1 C13 1250 - 400 300 40 3200 1100 4 4 16 1 x 0.111 300 * 8-100
C16 1250 - 400 300 40 3200 1100 4 i 16 1 x 0.111 300 * 8-100
C20 1250 - 400 300 40 3200 1100 4 4 16 2 x 0.111 300 * 8-100
C2 C23 1250 - 400 300 40 3200 1100 4 i 16 2 x 0.111 300 * 8-100
C26 1250 - 400 300 40 3200 1100 4 4 16 2 x 0.111 300 4> 8-100
* Beam D1, D2, D3, and D4 are corresponding to the specimen C35-90-80-1-2, C35-90-80-2-2, C35-90-30-1-2, and C30-90-80-1-2 named in Li et al. [49], respectively. The dia. is the diameter of the rebar, and 5 is the space between adjacent stirrups.
Table 2. Material properties (MPa).
Series Concrete Rebar Stirrup FRP
fc * ft Es fy fu Es fyv fu Ef fu
A1, A2 13.4 1.54 200,000 381 452 207,000 276 375 235,000 3,350
B1, B2 16.7 1.78 200,000 381 452 207,000 276 375 235,000 3,350
C1, C2 35.5 2.74 200,000 381 452 207,000 276 375 235,000 4,150
D1, D2, D3 23.4 2.20 200,000 378 447 205,000 235 362 243,000 4,390
D4 20.1 2.01 200,000 378 447 205,000 235 362 243,000 4,390
*f,f are the compression and tensile strength of concrete; Es, f, and f are Young's modulus, yielding strength, and ultimate strength of steel rebar; Es, fyv, and fu are Young's modulus, yielding strength, and ultimate strength of stirrup; Ef andfu are Young's modulus and ultimate strength of FRP reinforcement, respectively.
4. Results and Discussion
4.1. Test Results
The maximum bending moment and the shear force on the cross section of FRP-strengthened RC beam at initial debonding of FRP laminates are listed in Table 3.
There are 22 FRP-strengthened RC beams in series A1, A2, B1, B2, C1, and C2. 19 of them failed by IC debonding, their debonding process and characteristics are all the same. Taking beam A18 as an example, the debonding procedure and its characteristics are stated as follows.
The first flexural crack occurred when the applied load reached 10.0 kN. As the applied load was 31.7 kN, there are five flexural cracks developed at the constant moment region and eight flexure-shear cracks distributed at the shear spans and one of the flexure-shear cracks near the loading point became the critical flexure-shear crack (CFSC), as shown in Figure 2a. This applied load was constantly sustained, and FRP sheets were sequentially bonded on the tension face of RC beam. After the epoxy solidified, the test was continued. When the applied load reached 48.2 kN, the tension rebar yielded; the amount of cracks remains unchanged, but the width of the main flexural crack augmented slightly. Hereafter, the width of the CFSC was more pronounced with the increase of deflection. When the applied load reached 55.7 kN, one or two tributary cracks (TC) initiated in front of the CFSC towards the direction of decreasing moment, as shown in Figure 2b. The tributary cracks propagated towards the CFSC and intersected with it finally. In addition, the width of the TC was also increased with the increase of deflection, as shown in Figure 2c. When the applied load reached 60.6 kN, debonding initiated at the tip of the TC. Moreover, it can be clearly observed that the moment curvature of the shear span and the constant moment region were not in continuity, as shown in Figure 2d. As we know, the plastic hinge will be formed in the vicinity of the CFSC after tension rebar yielding. It can be observed in experimental tests that the crack space, crack width, and crack depth of flexure-shear cracks are all less than that of the flexural cracks. This indicates that the flexural stiffness of beam section at the shear span is higher than that at the constant moment region. As a result, the shear span of the beam will be rotated around the CFSC section leading to the discontinuity of moment curvature of RC beam left and right of the CFSC section, and was associated with the formation of relative vertical displacement between the two halves of the CFSC section. Figure 3 illustrates the relative vertical displacement between the two halves of the CFSC section.
Table 3. Test results and statistical analysis results.
Series Beam Tested Results Analyzed Results Vn/Vd Vn/Vd Vn/VMn Vn/VMn Md/Mn Md/Mn
* Md Vd Mn Vn VMn CoV CoV CoV
A20 24.9 33.2 23.5 81.3 31.4 2.45 2.59 1.06
A2 A23 A26 26.1 25.5 34.8 34.1 22.9 22.3 81.3 81.3 30.5 29.7 2.34 2.39 2.43 3.1% 2.66 2.74 2.70 3.2% 1.14 1.15 1.11 3.1%
A28 24.0 32.0 21.6 81.3 28.8 2.54 2.82 1.11
B20 31.4 41.8 33.0 105.1 44.0 2.51 2.39 0.95
B2 B23 B26 36.2 36.0 48.3 48.1 32.5 32.0 105.1 105.1 43.3 42.6 2.18 2.19 2.31 6.0% 2.43 2.47 2.45 1.8% 1.11 1.13 1.06 6.6%
B28 33.6 44.8 31.5 105.1 42.0 2.35 2.51 1.07
C10 136.5 109.2 155.0 223.4 124.0 2.05 1.80 0.88
C1 C13 125.3 100.2 153.7 223.4 123.0 2.23 2.19 4.6% 1.82 1.82 0.6% 0.81 0.83 4.1%
C16 122.5 98.0 152.6 223.4 122.1 2.28 1.83 0.80
C20 136.4 109.1 197.2 223.4 157.8 2.05 1.42 0.69
C2 C23 136.4 116.5 194.7 223.4 155.8 1.92 1.96 3.2% 1.43 1.43 1.0% 0.75 0.73 4.0%
C26 145.6 116.8 192.6 223.4 154.0 1.91 1.45 0.76
D1 15.8 26.3 16.0 61.2 26.6 2.33 2.30 0.99
D D2 D3 16.1 16.1 26.9 26.9 17.9 15.4 61.2 61.2 29.9 25.6 2.27 2.28 2.28 1.7% 2.05 2.39 2.28 6.0% 0.90 1.05 1.00 6.5%
D4 16.1 26.9 16.0 59.8 26.6 2.27 2.37 1.07
*Md, Vd are the maximum bending moment and the shear force on the cross section of FRP-strengthened RC beam at initial debonding of FRP laminates, Mn, Vn are the nominal flexural strength and shear strength of RC beam, V^ is the shear force on the cross section as RC beam reaches its nominal flexural strength Mn, ^ is the average of statistical variable, and CoV is the coefficient of variation of the statistical variable.
Figure 2. Debonding process and characteristics of beam A18 (a) Flexural cracks (FC-1-FC-5) and critical flexure-shear crack (CFSC). (b) Tributary crack (TC) generated near the tip of CFSC. (c) Debonding initiated at the tip of TC and deflection discontinuity left and right of the CFSC section. (d) Deflection discontinuity left and right of the CFSC section is very clear after FRP laminates totally debonded from concrete substrate.
Figure 3. Relative vertical displacement between two sides of the main crack [44-46].
Relative Displacement
It was observed during the test that the earlier initiation and more opening-up of CFSC, the earlier development of tributary cracks and the debonding of CFRP laminate. The present experimental results proved further that the shear resistance has an important effect on FRP debonding.
As it is well-known, the shear resistance of the beam section plays the key role in the opening-up of the CFSC and the relative vertical displacement between the two halves of the CFSC section. The greater the CFSC was opening-up, the greater the tensile stress concentrated in FRP composites, and the greater the shear stress produced on the FRP-concrete interface. Moreover, the relative vertical displacement between the two halves of the CFSC section makes the FRP composites produce normal tensile stress on the concrete substrate. Both the increase of the shear stress on the FRP-concrete interface and the normal tensile stress on the concrete substrate will promote the debonding of FRP laminates. Therefore, it can be concluded qualitatively that the shear capacity of RC beam plays a key role in debonding failure of RC beams flexurally strengthened with externally bonded FRP composites.
4.2. Influence of Shear Resistance of RC Beam on Flexural Debonding Load-Carrying Capacity
In addition to the test results of series A2, B2, C1, and C2, the test results of series D carried out by Li et al. [49] are also analyzed as a supplement of the limited test results. All the strengthened beams in series D failed by IC debonding. The dimensions and materials properties of series D are listed in Tables 1 and 2.
Whether the flexural failure or the shear failure depend on the internal forces, that is, the bending moment and the shear force, on the cross section of RC beam. To make the analytical results of the influence of shear resistance on flexural debonding load-carrying capacity of FRP-strengthened RC beams comparable, the ratio of nominal shear strength Vn to shear force Vd on the critical section at initial debonding, Vn/Vd, was used. Similarly, to make the analytical results comparable in evaluating the flexural debonding load-bearing capacity, the ratio of tested debonding bending moment Md to the nominal flexural strength Mn of the strengthened beam, Md/Mn, was used. Then, the influence of shear resistance Vn/Vd on flexural debonding load-bearing capacity Md/Mn was analyzed based on the test results. The nominal shear strength and flexural strength of FRP-strengthened RC beams are calculated according to the conventional RC theory.
The nominal shear strength of RC beam is calculated by the formula provided by GB20010-2010 [50]:
Vn = TZ7 fb bd0 + fyv — do (1)
Where, f is the tensile strength of concrete; fyv is the yield strength of stirrup steel, b and d0 are the width and effective depth of beam section, X is the depth-span ratio of beam, s is the spacing of shear reinforcement, and Asv is the total cross-sectional area of stirrup within a distance s, respectively.
The nominal flexural strength of FRP-strengthened RC beam is calculated by provisions in ACI440-08 [29]:
M n = Afy (d - "Y )+A ffe ( d - ) (2)
Where, As and Af are the total cross-sectional area of tension steel and FRP reinforcements, d is the total depth of beam cross-section, c is the distance from the outer compressive fiber to the neutral axis,
is a constant that is a function of the compressive strength of concrete, fy is the yield strength of tension steel, and fe is the effective tensile stress in FRP reinforcement, and:
ffe = Ef 8 fe (3)
fe = ^cu(-) - ^bi (4)
Where, Ef is the modulus of elasticity of FRP composite, Sfe is the effective tensile strain in FRP reinforcement, scu is the ultimate compressive strain of concrete, and sbi is the initial strain level on the bonded substrate, it can be determined from an elastic analysis of the existing member, considering all loads that will be on the member during the installation of the FRP system.
Table 3 summarizes the maximum bending moment Md and the shear force Vd on the cross section of FRP-strengthened beam at initial debonding of FRP laminates, the nominal flexural strength Mn and shear strength Vn, and the shear force VMn on the cross section as the RC beam reaches its nominal flexural strength Mn.
Their average |i and coefficient of variation CoV of Vn/Vd, Vn/VMn and Md/Mn were analyzed and summarized in Table 3.
The averages of Md/Mn of series A2, B2, C1, C2, and D are 1.11, 1.06, 0.83, 0.73, and 1.00, with coefficients of variation of 3.1%, 6.6%, 4.1%, 4.0%, and 6.5%, respectively. The averages of Vn/Vd of series A2, B2, C1, C2, and D are 2.43, 2.31, 2.19, 1.96, and 2.28, with coefficients of variation of 3.1%, 6.0%, 4.6%, 3.2%, and 1.7%, respectively. Figure 4 shows the relationship between Md/Mn and Vn/Vd, their goodness of linear fit R2 is 0.9134. This indicates that Md/Mn and Vn/Vd have a good linear relationship. When Vn/Vd is 1.96, Md/Mn is 0.73. However, Md/Mn is 1.11 as Vn/Vd is 2.43. It is obviously that the flexural debonding load-carrying capacity is significantly increased with the increase of Vn/Vd. Md/Mn is only 0.73 as Vn/Vd is 1.96, this indicates that debonding failure will be initiated when the bending moment Md on the cross section is much lower than its nominal flexural strength Mn. However, when Vn/Vd is greater than 2.28, the ratios of Md/Mn are all greater than 1.0, this implies that debonding failure will not occur when the bending moment on the cross section reaches the nominal flexural strength of FRP-strengthened RC beam. Therefore, it can be concluded that the shear resistance of RC beam has a great effect on flexural debonding load-carrying capacity of
FRP-strengthened RC beam. As a result, the influence of shear resistance on flexural debonding load-carrying capacity must be fully considered in the flexural strengthening design of RC beams.
Figure 4. Relationship between Vn/Vd and Md/Mn.
1.20 un
1.10 R2 = 0.9134^ • /
1.00 -
0.90 -
0.80 -
0.70 - m/
0.60 lyld
1.80 2.00 2.20 2.40 2.60
However, the shear force Vd on the cross section cannot be determined in flexural strengthening design of RC beams. Consequently, the relationship between Vn/Vd and Md/Mn cannot be used in flexural strengthening design. In order to take the influence of shear resistance on flexural debonding load-carrying capacity into account in flexural strengthening design of RC beam, the shear force VMn which is the shear force on the cross section as RC beam reaches its nominal flexural strength Mn substituting for Vd was employed to analyze the relationship between Vn/VMn and Md/Mn. Table 3 shows the statistical analysis results. The averages of Vn/VMn of series A2, B2, C1, C2, and D are 2.70, 2.45, 1.82, 1.43, and 2.28, with coefficients of variation of 3.2%, 1.8%, 0.6%, 1.0%, and 6.0%, respectively. Figure 5 shows the relationship between Md/Mn and Vn/VMn, their goodness of linear fit R2 is 0.9919. This indicates thatMd/Mn and Vn/VMn have a very good linear relationship and have the same variation tendency as Vn/Vd and Md/Mn. Therefore, the relationship between Md/Mn and Vn/VMn can also be used in evaluating the influence of shear resistance on flexural debonding load-carrying capacity, and thus provides support for flexural strengthening design. According to the statistical analysis results of Md/Mn and Vn/VMn, when Vn/VMn is greater than 2.28, the ratios ofMd/Mn are all greater than 1.0. Therefore, it is suggested that Vn/VMn should not be less than 2.3. This limitation ensures that debonding of FRP reinforcements will not be initiated as FRP-strengthened RC beam reaches its nominal flexural strength.
Figure 5. Relationship between Md/Mn and Vn/ VMn.
5. Conclusions
This present study investigates and analyzes the effect of shear resistance on flexural debonding load-carrying capacity of FRP-strengthened RC beams based on the test results. Within the scope of the limited experimental results, the following conclusions can be drawn from this study:
• The shear resistance of RC beam has a great effect on flexural debonding load-carrying capacity of FRP-strengthened RC beam. The influence of shear resistance on flexural debonding load-carrying capacity must be fully considered in flexural strengthening design of RC beams.
• Md/Mn and Vn/Vd have a good linear relationship. The flexural debonding load-carrying capacity is significantly increased with the increase of Vn/Vd. The goodness of the linear fit of Md/Mn and Vn/VMn is better than that of Md/Mn and Vn/Vd, and their variation tendency is the same. Therefore, the relationship between Md/Mn and Vn/VMn can also be used in evaluating the influence of shear resistance on flexural debonding load-carrying capacity, and also provides support for flexural strengthening design. It is suggested that Vn/VMn should not be less than 2.3 in order to prevent debonding failure of FRP reinforcements as FRP-strengthened RC beam reaches its nominal flexural strength.
• The existing debonding models were developed based on the single-shear test results. However, the experimental results proved that the shear resistance of RC beam plays the key role in FRP debonding failure. Consequently, the influence of shear resistance of RC beam on FRP debonding failure must be fully considered in developing the debonding criteria and model.
• Presently, only a few of experimental studies have been carried out against investigating the influence of shear resistance on flexural debonding load-carrying capacity of FRP-strengthened RC beams. This vital issue, which remains under investigated, must be given the attention it deserves through further experimental and analytical studies.
Acknowledgments
The authors wish to acknowledge the staff members in the Structure Laboratory of Zhejiang University for their necessary support to carry out the tests. We would also like to express our gratitude to the following graduate students Xiaolong Xu, Jin Zhou, and Dengfeng Zhou, for their assistance in conducting the experimental phases of this study and to thank the reviewers for their careful review and constructive suggestions and to thank the Assistant Manager Jingjing Yang for her careful editing with regard to our manuscript.
This research project has been partially funded by the science and technology development foundation for college and university in Shanghai (03HK03).
Author Contributions
Guibing Li is responsible for performing the mechanical tests and has contributed to the writing of all the sections within the paper. Aihui Zhang is working on directing the mechanical tests and has been in charge of writing the results and discussion and conclusions sections to analyze the results. Weiliang Jin is responsible for the research project.
Conflicts of Interest
The authors declare no conflict of interest.
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