Shear Behaviour of RC Beams Strengthened by Various Ultrahigh Performance Fibre-Reinforced Concrete Systems

Mansour, Walid; Tayeh, Bassam A.

doi:https://doi.org/10.1155/2020/2139054

Advances in Civil Engineering

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Research Article | Open Access

Volume 2020 | Article ID 2139054 | https://doi.org/10.1155/2020/2139054

Shear Behaviour of RC Beams Strengthened by Various Ultrahigh Performance Fibre-Reinforced Concrete Systems

Walid Mansour¹and Bassam A. Tayeh²

Academic Editor: Raffaele Landolfo

Received20 Jan 2020

Revised30 Mar 2020

Accepted29 Jun 2020

Published16 Jul 2020

Abstract

This study presents a numerical investigation on the shear behaviour of shear-strengthened reinforced concrete (RC) beams by using various ultrahigh performance fibre-reinforced concrete (UHPFRC) systems. The proposed 3D finite element model (FEM) was verified by comparing its results with those of experimental studies in the literature. The validated numerical model is used to analyse the crucial parameters, which are mainly related to the design of RC beams and shear-strengthened UHPFRC layers, such as the effect of shear span-to-depth ratio on the shear behaviour of the strengthened or nonstrengthened RC beams and the effect of geometry and length of UHPFRC layers. Moreover, the effect of the UHPFRC layers’ reinforcement ratio and strengthening of one longitudinal vertical face on the mechanical performance of RC beams strengthened in shear with UHPFRC layers is investigated. Results of the analysed beams show that the shear span-to-depth ratio significantly affects the shear behaviour of not only the normal-strength RC beams but also the RC beams strengthened with UHPFRC layers. However, the effect of shear span-to-depth ratio has not been considered in existing design code equations. Consequently, this study suggests two formulas to estimate the shear strength of normal-strength RC beams and UHPFRC-strengthened RC beams considering the effect of the shear span-to-depth ratio.

1. Introduction

Many reinforced concrete (RC) structures have to be repaired or strengthened to address their limitations in structural performance and/or durability properties [1]. The need to strengthen can be due to many reasons, such as change in service conditions, corrosion of steel reinforcement, or upgradation of current design code provisions. A promising material used in the strengthening of RC structures is the ultrahigh performance fibre-reinforced concrete (UHPFRC) because of its superior mechanical properties, very high strength in compression and tension, and extremely densified microstructure. The mechanical properties of UHPFRC have been extensively investigated [2–9].

In the last decade, studies have experimentally used UHPFRC for the flexural strengthening of RC beams [10–14]. They showed that UHPFRC could increase stiffness and resistance and delay the formation of localised cracks. In addition, Al-Osta et al. [15] explored the effectiveness and efficiency of strengthening RC beams with UHPFRC by (a) roughening the surface of RC beams via sand blasting and casting the UHPFRC in situ around the beams and (b) joining the prefabricated UHPFRC plates to the RC beams using epoxy. However, Tayeh et al. [16] investigated the strengthening of RC beams with UHPFRC laminates using the two different bonding methods of gluing with epoxy and mechanical anchoring. The aforementioned techniques emphasised that beams strengthened with a three-side jacket showed the highest capacity enhancement, whereas beams strengthened only at the bottom soffit showed lower enhancement [15, 16]. Moreover, the flexural response of strengthened RC beams improved when reinforcing bars were added within the laminates.

The technique of flexural strengthening using UHPFRC was investigated numerically in [17] by developing a numerical model for the extensive investigation of strengthened RC beams with layers and jackets. Their findings were compared with those of beams strengthened with conventional RC layers and combinations of UHPFRC and steel-reinforcing bars. Their results clearly showed that superior performance could be achieved by using the three-side UHPFRC jackets.

Shear failure is unfavourable for engineers because of its sudden occurrence with a brittle failure mode, and many studies have focused on improving the capacity and ductility of RC beams strengthened in shear with UHPFRC [13, 18–22]. Sakr et al. [23] proposed a 3D finite element model (FEM) to investigate the behaviour of RC beams strengthened in shear with prefabricated UHPFRC plates by using (a) one longitudinal vertical-side strengthening and (b) two longitudinal vertical-side strengthening. They concluded that the prefabricated UHPFRC plates could significantly enhance the ultimate load carrying capacity, ductility, and strain of longitudinal reinforcement in the strengthened RC beams compared with the control beam failed in shear.

Moreover, Mohammed et al. [24] experimentally and numerically examined the effectiveness and efficiency of UHPFRC-strengthened RC beam specimens without stirrups by using three different strengthening techniques under torsional moment. The beam specimen strengthened on all four sides obtained higher torsional strength compared with the reference specimen.

Despite the results of these studies using UHPFRC in strengthening and rehabilitating conventional RC beams, limited studies have considered the effect of the shear span-to-depth and UHPFRC layer reinforcement ratios on the behaviour of RC beams strengthened in shear with UHPFRC. Moreover, information on the effect of UHPFRC layer length and geometry on the behaviour of the considered structure is lacking. Because of the difficulty of strengthening many structural elements on both sides especially in exterior beams due to the neighbouring borders, strengthening the RC beams using only one vertical longitudinal side has been considered in the current research. Strengthening only one vertical longitudinal side of the RC beams is rarely studied and evaluated in the literature.

Thus, a 3D FEM with the ability to simulate the behaviour of RC beams strengthened in shear with UHPFRC layers is proposed in this study and validated using the experiments available in the literature (Sections 2 and 3). Additionally, the validated FEM is used in Section 4 to demonstrate the effects of the shear span-to-depth ratio, length, and geometry of UHPFRC layers, reinforcing UHPFRC layers and strengthening only one longitudinal vertical side on the behaviour of RC beams strengthened in shear with UHPFRC layers.

2. Numerical Investigation

The shear behaviour of simply supported RC beams strengthened with UHPFRC using different strengthening schemes was investigated numerically. The nonlinear finite element analysis software ABAQUS [25] was used to develop a 3D model simulating the shear behaviour of UHPFRC-strengthened RC beams.

2.1. Elements and Meshing

Normal-strength concrete (NSC) and UHPFRC are modelled using the 3D stress eight-noded linear brick element (C3D8R), as shown in Figure 1. This figure also shows the two-noded linear 3D truss element (T3D2), which is used to model the steel-reinforcing bars and stirrups. This element is suitable for structural members that transmit only axial load.

(a)

(b)

(c)

A mesh size of 40 mm × 40 mm was suggested to divide the simulated RC beams to fine elements. The proposed fine mesh was required to obtain accurate results consistent with those of the experimental response on the level of failure load and failure pattern.

2.2. Materials

The model of concrete damage plasticity was used to simulate both concrete and UHPFRC although two other models (concrete smeared and brittle cracking) were available in ABAQUS. The model of concrete damage plasticity was used in this study due to its ability in modelling the complex nonlinear properties of concrete and UHPFRC considering the softening behaviour under either compression or tension. This approach can also be used with a rebar to model concrete reinforcement.

The model of concrete damage plasticity assumes that the uniaxial tensile and compressive response of concrete is characterised by damaged plasticity, as illustrated in Figure 2. The damage variables in compression and tension were denoted by d_c and d_t, respectively. Such damage variables can take values from 0 (to represent the undamaged material) to 1 (to denote the total loss of strength). In the case of uniaxial tension, the stress-strain response followed a linear elastic relationship until the value of the failure stress, , was reached. Beyond the failure stress, the formation of microcracks was represented macroscopically with a softening stress-strain response, which induced strain localisation in the concrete structure. The response was linear under uniaxial compression until the value of the initial yield, , was reached. The response in the plastic zone was typically characterised by stress hardening, followed by strain softening beyond the ultimate stress, . Birtel and Mark [26] proposed the following equations to determine the compressive and tensile damage parameters:(i)Compressive damage parameter (d_c):(ii)Tensile damage parameter (d_t): where d_c and d_t are the compressive and tensile damage parameters, respectively; σ_c and σ_t are the compressive and tensile stresses of concrete, respectively; E_c is the elasticity modulus of concrete; and are the plastic strains corresponding to the compressive and tensile strengths of concrete, respectively; and b_c and b_t are constant parameters (they can take values from 0 to 1).

(a)

(b)

The reinforcement steel was modelled using elastic-perfectly plastic material, as suggested in [23]. The relationship between the reinforcement steel and concrete was modelled as a perfect bond (embedded region, whereas the concrete was the host element).

3. Numerical Validation

The results of the proposed FEM were compared with the experimental results available in the literature [21] to verify its accuracy. The experimental investigation consisted of nine RC beams prepared considering the shear span-to-depth ratio (a/d) and strengthening pattern as two variable parameters. Two steel rebars with 20 mm diameter were placed in the tension zone, whilst two rebars with 12 mm diameter were provided in the compression zone of all the specimens. Moreover, two-legged stirrups with 8 mm diameter at a spacing of 120 mm were used as shear reinforcement. Table 1 lists the details of the nine beam specimens. This table concluded that the beam specimens were strengthened by applying a 30 mm layer of UHPFRC over the longitudinal vertical faces of the RC beam specimens. UHPFRC jacketing was executed in the following schemes: (a) two longitudinal vertical faces of the beams and (b) two longitudinal vertical faces in addition to the bottom face.

The materials of concrete, UHPFRC, and steel reinforcement were modelled using the data generated through the experimental program, as shown in Table 2.

The model parameters of concrete damage plasticity for concrete and UHPFRC materials are defined in Table 3, whereas the simulated nonlinear properties of both concrete and UHPFRC under tension and compression are depicted in Figure 3.

(a)

(b)

Table 4 shows the number of elements, number of degrees of freedom, and central processing unit time. The processor type used for this study was 2.4 GHz with core i7.

The bond between NSC and UHPFRC was considered a perfect bond (tie constraint; the concrete and UHPFRC are the master and slave surfaces, respectively) because debonding was not observed in all the experimental tests [27–32]. The control and strengthened beam specimens were analysed under a four-point loading arrangement. All experimental results, including failure load, failure mode, and load-deflection responses, were compared with those obtained through numerical modelling to check their validity.

3.1. Load-Deflection Responses

The load-deflection responses of FE obtained for the control beams, beams strengthened using two layers, and beams strengthened using three-side jackets with different shear span-to-depth ratios are shown in Figures 4–6, respectively, and compared with the experimental results.

The results showed that FEM could simulate the behaviour of the RC control beams in addition to the RC beams strengthened with UHPFRC with acceptable accuracy.

Table 5 presents a comparison between the experimental results of ultimate load and deflection at maximum load and their counterparts obtained using FE analysis. For the first group (control specimens), the experimental value of failure loads for CT-1.0, CT-1.5, and CT-2.0 were 383, 286, and 276 kN versus the predicted 379, 295, and 285 kN through the numerical model with a difference of only 1%, 3%, and 3%, respectively. Additionally, FEM could obtain the ultimate load for the strengthened RC beams SB-2SJ-1.0, SB-3SJ-1.0, SB-2SJ-1.5, SB-3SJ-1.5, SB-2SJ-2.0, and SB-3SJ-2.0 with a difference of 1%, 1%, 2%, 0%, 8%, and 1%, respectively, compared with the experimental results, which had acceptable accuracy. The numerical model can accurately estimate not only the ultimate load but also the midspan deflection at maximum load. The experimental midspan deflections for the tested RC beams were in the range of 2.17 to 7.50 mm compared with 2.70 to 9.00 mm in the case of FEM.

3.2. Failure Mode

The experimental and numerical investigations showed that control beams CT-1.0, CT-1.5, and CT-2.0 failed in shear compression by forming diagonal cracks joining the points of the load application and support, as shown in Figures 7–9, respectively. In the case of beam specimens SB-2SJ-1.0, SB-2SJ-1.5, and SB-2SJ-2.0, the vertical flexural cracks appeared at the beam midspan, followed by the inclined crack, as depicted in Figures 10–12, respectively. However, beam specimens SB-3SJ-1.0, SB-3SJ-1.5, and SB-3SJ-2.0 failed in the flexure by forming vertical cracks located in the maximum bending moment zone, as depicted in Figures 13–15, respectively. This comparison concluded that FEM could successfully simulate the majority of failure modes.

(a)

(b)

(a)

(b)

(a)

(b)

(a)

(b)

(a)

(b)

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(b)

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(b)

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4. Parametric Study

The validated FEM was used in the numerical investigation of the crucial parameters related to the design of RC beams strengthened in shear with UHPFRC layers. The effect of parameters and the geometry and length of UHPFRC layers on the shear span-to-depth ratio and shear behaviour of RC beams were determined. In addition, the effects of UHPFRC layers’ reinforcement ratio and one longitudinal vertical face strengthening on the mechanical performance of RC beams strengthened in shear with UHPFRC layers were demonstrated.

4.1. Shear Span-to-Depth Ratio

4.1.1. Control Beam Specimens

Previous studies [33–39] have shown that the shear span-to-depth ratio significantly affects the shear behaviour of RC elements. However, this term has been ignored in current design code equations [40, 41], which estimate the shear capacity of RC beams. Eleven normal-strength RC beams with shear span-to-depth ratios ranging from 1.0 to 3.5 at 0.25 intervals were analysed using the validated FEM, as shown in Table 6. Such samples helped not only to understand the performance of RC members with different ratios of shear span-to-depth ratio but also derive an equation estimating the shear capacity of RC beams considering the effect of shear span-to-depth ratio. The results presented in Table 6, including the ultimate load besides deflection at ultimate load, reveal that the ultimate load decreases as the shear span-to-depth ratio and deflection increase. As the shear span-to-depth ratio increased, the shear failure mode gradually changed from shear-compression failure to shear-tension failure. Shear cracks propagated rapidly and violently in the shear-tension failure, thereby causing the deterioration in ultimate load with the increase in shear span-to-depth ratio.

The ultimate load of the analysed specimens was calculated using the following design codes [40, 41].

(1) Euro Code 2 (EC2). The Euro code estimates the shear resistance of beams with stirrups, , as follows:where ; is the cylinder compressive strength of concrete, MPa; d is the effective depth, mm; is the longitudinal reinforcement ratio; b is the beam width, mm; is the cross-sectional area of shear reinforcement; is the spacing of stirrups; is the design value of the steel yield strength; and is the design concrete strut angle.

The value of may be set to , whereas the internal lever arm may be set to [42]. Additionally, the long-term coefficient factor is set to 0.85, as recommended in [43].

(2) ACI Code. ACI code considers both the concrete and shear reinforcement contributions when the shear capacity is calculated as

The obtained results in numerical ultimate load versus ultimate load using the aforementioned design codes for the 11 specimens are shown in Figure 16.

The EC2 and ACI codes failed to capture the response of the RC beams compared with FEM. Their values are always constant despite the change in shear span-to-depth ratios because this term was ignored in their calculations. Moreover, the ACI code obtained lower estimates than EC2 in the ultimate load of the analysed RC beams because a diagonal concrete strut () of 45° was adopted in the ACI model compared with in the case of the EC2 model. A new equation that can predict the ultimate load of the RC beams considering the effect of shear span-to-depth ratio is necessary to improve the accuracy of the current design code equations. A new equation was derived on the basis of nonlinear regression analysis of the numerical results using SPSS statistics program, and its results were compared with those of the numerical and analytical models, as shown in Table 7.

(3) New Equation. The proposed new equation estimates the shear capacity of concrete members considering the concrete compressive strength and effect of shear span-to-depth ratio () as follows:

The proposed new equation estimated the ultimate load capacity of RC control beams well by using the numerical model with an average error of 6.34%, as shown in Table 7. However, further experimental and numerical studies are required to improve the accuracy of the proposed equation.

4.1.2. RC Beam Specimens Strengthened with UHPFRC Layers

Table 8 presents the effect of shear span-to-depth ratio on the ultimate load and deflection at the ultimate load of RC beams strengthened with UHPFRC on (a) two longitudinal vertical faces of beams (series SB-2SJ) and (b) two longitudinal vertical faces in addition to the bottom face (series SB-3SJ). The ultimate load of the strengthened RC beams decreased significantly with the increase in shear span-to-depth ratio. In the case of SB-2SJ series, the ultimate load decreased from 560 kN in the case of SB-2SJ-1.0 specimen to 175 kN in the case of SB-2SJ-3.5 with a decreasing ratio of 68%. Strengthening the vertical and bottom faces of the RC beams (series SB-3SJ) still deteriorated the ultimate load with the increase in shear span-to-depth ratio. The ultimate load was 631 kN and 196 kN in the SB-3SJ-1.0 and SB-3SJ-3.5 specimens, respectively, with a decreasing ratio of 69%. By contrast, the shear span-to-depth ratio increased as the deflection at ultimate load increased due to the superior mechanical properties of UHPFRC in tension from the crack bridging phenomena, which occurred because of the presence of steel fibre.

4.2. Geometry and Length of UHPFRC Layers

This section investigated the effect of the strengthening pattern and strengthening length on the shear response of the RC beams strengthened with UHPFRC layers. Ten RC beams were strengthened via (a) strengthening with UHPFRC strips spaced every 100 mm and (b) strengthening using UHPFRC layers. The results are listed in Table 9. The following nomenclature was used to distinguish between the two technical specimens: SB-2SJ-ST-100: the specimen strengthened with UHPFRC strips where the third and fourth items were ST = strips and width of the UHPFRC strip = 100 mm, respectively (Figure 17). SB-2SJ-0.33L: the specimen strengthened with a UHPFRC layer, where the third item is the length of the UHPFRC layer as a ratio from the beam length (L) and equal to 0.33L (Figure 18).

(a)

(b)

(a)

(b)

In the RC beams strengthened using two longitudinal vertical faces of UHPFRC, as expected, specimen SB-2SJ-2.0 was fully strengthened over its length and obtained the highest ultimate load and deflection at 317 kN and 9.00 mm, respectively. However, specimen SB-2SJ-0.33L with the lowest strengthening length realised the lowest ultimate load (287 kN) with an increasing ratio equal to only 0.7%, as compared with the reference beam CT-2.0. Additionally, specimen SB-2SJ-0.74L (strengthened along the shear zones only) improved the failure load by 5.60%, whereas the control beam CT-2.0 obtained 5.90 mm deflection at the ultimate load.

In the case of specimens strengthened on both vertical faces and lower face using UHPFRC, the ultimate load capacity increased as the strengthening length increased. Specimen SB-3SJ-2.0 obtained the highest ultimate load and deflection at 356 kN and 7.20 mm, respectively, whereas specimen SB-3SJ-0.33L achieved the lowest ultimate load (314 kN), which was 10.20% higher than that of specimen CT-2.0. Beam SB-3SJ-0.74L failed at 341 kN with an increasing ratio of 19.70% compared with that of the control specimen. This finding indicated that the design engineers should strengthen the entire length of the RC beam with UHPFRC layers. This strengthening technique demonstrated the highest ultimate load with sufficient deflection.

4.3. Reinforcing UHPFRC Layers

To increase the ultimate load and ductility of the strengthened RC beams, we used UHPFRC layers with reinforcement bars (Figure 19) for external strengthening with different reinforcement ratios, as shown in Table 10.

As expected, the first group (vertically strengthened) reinforcing the UHPFRC vertical layers in the case of beam SB-2SJ-2.3-3.6 increased not only the ultimate load by 14%, compared with specimen SB-2SJ-2.0, but also the deflection at ultimate load by 22%. Beam SB-2SJ-7.4-3.6 with the largest reinforcement ratio obtained the highest ultimate load at 516 kN, whereas specimen SB-2SJ-2.0 obtained an ultimate load of 317 kN. The use of reinforced UHPFRC layers improved not only the ultimate load and deflection at ultimate load but also the failure mode manifested as flexural cracks, as shown in Figure 20. As a result, increasing the transversal reinforcement ratio within the UHPFRC layers did not significantly improve the ultimate load capacity of the strengthened specimens. Moreover, reinforcement helped in the uniform distribution of stresses occurring on the surface of the strengthened RC beams and resulted in large deformations at failure.

However, specimen SB-3SJ-7.4-8.5 from the second group (strengthening vertical faces in addition to the lower face) obtained the largest ultimate load amongst all the strengthened RC specimens at 673 kN, whereas beam specimen SB-3SJ-2.0 achieved an ultimate load of 356 kN. Moreover, specimens SB-3SJ-2.3-2.6, SB-3SJ-3.3-3.8, and SB-3SJ-5.8-6.7 obtained higher ultimate load at 38%, 58%, and 80%, respectively, compared with specimen SB-3SJ-2.0.

4.4. Strengthening of One Longitudinal Vertical Face

Strengthening two longitudinal vertical faces of the RC beams may not be available at all times, especially in exterior beams due to the neighbouring borders. Nine strengthened RC beams were divided into two groups. The first contained five RC beams, which were strengthened using a nonreinforced UHPFRC layer with different strengthening lengths, whereas the second group adjoined four RC beams, which were strengthened over the entire length by using a reinforced UHPFRC layer with different reinforcement ratios, as demonstrated in Table 11. Additionally, the RC control beam CT-2.0 was imported within the table for comparison with the strengthened RC beams. Notably, only the surface of the RC beam without the UHPFRC layer was loaded and supported to simulate the real structure case of the strengthened RC beams.

Regarding the first group, beams SB-1SJ-ST-100, SB-1SJ-ST-200, SB-1SJ-0.33L, SB-1SJ-0.74L, and SB-1SJ-2.0 failed completely in shear (Figure 21) at a load of 289, 290, 287, 293, and 300 kN compared with the control RC beam CT-2.0 at 285 kN. No significant increase occurred in the ultimate load but stiffness improved significantly. The use of a reinforced UHPFRC layer in the second group improved the shear response and stiffness. Beams SB-1SJ-2.3-3.6, SB-1SJ-3.3-3.6, SB-1SJ-5.8-3.6, and SB-1SJ-7.4-3.6 failed at the load values of 318, 328, 352, and 376 kN, whereas the control RC beam with sufficient deflection at ultimate load obtained a load value of 285 kN, as shown in Figure 22. Consequently, if one longitudinal vertical face of the RC beam is strengthened, then a reinforced UHPFRC layer is used to improve the shear response.

5. Conclusions

This study aims to propose FEM to simulate the behaviour of RC beams strengthened in shear by using various UHPFRC systems. The results of the numerical model and a previous study in the literature are compared to check the validity of the proposed FEM. The validated FEM is used to analyse the crucial parameters related to the design of RC beams strengthened in shear with UHPFRC layers. The main conclusions of this study are summarised as follows:(1)The shear behaviour of normal-strength RC beams and RC beams strengthened with UHPFRC layers is affected significantly by the change in the shear span-to-depth ratio. However, the effect of shear span-to-depth ratio has not been considered in current design code equations. Accordingly, design formulas are proposed for the estimation of shear strength of normal-strength RC beams and RC beams strengthened with UHPFRC considering the effect of the shear span-to-depth ratio.(2)When the UHPFRC strengthening length is changed, the highest ultimate load is obtained by strengthening the entire length of RC beams. The obtained ultimate load can be increased significantly by reinforcing the strengthening UHPFRC layers. Specimen SB-2SJ-7.4-5.7 failed at 511 kN compared with 317 kN in case of SB-2SJ-2.0 with sufficient ductility. However, the ultimate load of specimen SB-3SJ-7.4-8.5 was equal to 673 kN versus 356 kN for specimen SB-3SJ-2.0, which was strengthened using nonreinforced UHPFRC layers.(3)Strengthening RC beams with one longitudinal vertical face must be executed using a reinforced UHPFRC layer to improve the shear response of the strengthened RC beams.

Data Availability

The data used to support the findings of this study are included in the article.

Conflicts of Interest

The authors declare that they have no conflicts of interest.

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Copyright © 2020 Walid Mansour and Bassam A. Tayeh. 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.

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