Properties of Self-Compacting Concrete Produced with Optimized Volume of Calcined Clay and Rice Husk Ash—Emphasis on Rheology, Time Dependent Workability and Durability

1. Introduction

For decades, concrete has provided the infrastructure stood synonymous for economic growth and development, partly because of its peculiar mechanical and durability characteristics, ease of production and placement, and the wide availability of its constituents [1]. Concrete is a mixture of a binder (usually cement or a blend of cement and supplementary cementitious materials), coarse and fine aggregates, water and other admixtures that, when mixed and cured, becomes a robust stone-like material capable of withstanding the effects of deteriorative mechanisms such as the ingress of harmful chemicals, the freeze-thaw cycle, rain storms or other harsh environmental conditions [2,3].

Thus fore concrete requires a dense microstructure that can provide adequate cover to the embedded reinforcement bars and resist the ingress of harmful substances which could jeopardize the concrete itself. One possible way to ensure better compaction of the concrete and for filling all the corners of formwork and embedding the steel reinforcements is to adopt a self-compacting method of concrete production [4,5].

Self-compacting placement method ensures homogeneous deformation of the fresh concrete, under the influence of gravity, to fill all the gaps and corners of the formwork and embed the reinforcement bars, without the need for external vibration or compaction, thereby ensuring a homogeneous and dense hardened concrete microstructure with an excellent strength and durability [6]. The flowability of the self-compacting concrete (SCC) is achieved by proper optimization of the volumetric water-to-powder ratio (V_w/V_p) and the use high range water-reducing admixtures [7], while the homogeneity of the powder-type of SCC is achieved by an optimal proportioning of fine and coarse particles of the concrete constituents [6]. In this regard, the proportion of coarse aggregate is reduced while the volume of mortar in the system is increased. Consequently, the quantity of the powder required to achieve optimized fresh SCC properties (powder-type) is greater than that of the conventional vibrated concrete [8], making the concrete more expensive and less environmentally friendly.

One potential way to make SCC cost-effective and reduce the effects of excessive use of cement per m³ of SCC – such as shrinkage and high CO₂ emission - is to reduce the amount of cement per m³ of SCC. This can be achieved by partially replacing cement clinker with filler and/or supplementary cementitious materials (SCMs). The most commonly used natural filler in SCC is limestone powder (LP), which can replace up to 35 wt-% of cement clinker [9], thereby reduces cement interparticle friction and decreases the flow resistance of the SCC [10,11], and promotes the reaction of C₃S and the formation of AFm phases (hemi/monocarboaluminate) [12,13]. SCMs such as fly ash, silica fume, metakaolin, rice husk ash (RHA) and others can also be used as partial cement substitutes in SCC. Binary and ternary cement partial replacement with fly ash up to 30 wt-% improves the durability of SCC and reduces its drying shrinkage [14,15]. Higher cement partial replacement by fly ash will soon no longer be possible due to the decline in coal-combustion enforced to limit the global CO₂ release. Similarly, silica fume at 10 wt-% cement partial substitute improves compressive strength and durability of SCC [16,17], but its use at higher dosage is also limited due to its cost, high water demand and portlandite consumption.

CC are anhydrous aluminosilicate pozzolanic materials that can partially replace cement at high proportions and improved strength and durability of concrete. Metakaolin is the most reactive CC in concrete and mortar due to its higher early strength compared to other CCs [18,19,20]. However, due to its frequent use in other competing industries, metakaolin is an expensive material and less available compared to the other 2:1 CC. Although the relevance of other common CC for conventional vibrated concrete has been investigated in recent years [21,22], their application should also be extended to SCC. RHA, on the other hand, is a silica-rich SCM that can be used as a viscosity modifying agent or as a partial replacement to cement in SCC [20,23,24,25]. Its specific surface area and water demand exceed those of cement and metakaolin [20,23]. Therefore, similar to silica fume, its use in SCC is limited due to its effect on the deformability characteristics of SCC. Similar to the metakaolin, the use of RHA as a partial replacement to cement at 20 wt-% consumed the portlandite and enhances the precipitation of the C-S-H, thereby densifying the microstructure of SCC and improving its strength and durability [23,24,25].

SCC usually differs from conventional vibrated concrete only in its fresh properties. Its deformability characteristics and the workability retention are important attributes that determine its application. For instance, in the precast concrete plant, SCC can be cast into the forms about 10 to 30 minutes after mixing, and the time-dependent measurement of workability is not as important as in the ready-mix concrete, which often requires 30 to 120 minutes after mixing [26]. Although maintaining the workability of the SCC over an extended period of time is not readily achievable, it is important that the ready-mixed SCC still exhibit the required SCC fresh concrete properties at the time of placement. The deformability characteristics of SCC after mixing can be assessed by measuring the yield value (slump flow), which defines the flowability of the SCC, and by checking the deformation rate by V-funnel measurement as an indication of viscosity [27,28]. The SCC can then be finally analysed for its blocking and segregation tendency [29]. These properties are usually measured within 30 minutes of mixing and are not indicative of the long-term workability of the SCC. The time-dependent stability of SCC can be assessed by determining the immersion depth of the plunger in SCC in a cylindrical mould, as developed by FIZ (Research Institute of the Cement Industry) Düsseldorf [30], or by comparing the flow resistance of the SCC over time, calculated from the curves of shear stress versus shear rate from the rheological measurements.

It is obvious that both metakaolin and RHA at a certain cement replacement ratio densified the concrete microstructure, improving its chloride penetration resistance, increasing compressive strength, and decreasing drying shrinkage tendency, but both are known for their high specific surface area and high water demand both exceeding significantly those of cement [20]. Consequently, the flow resistance of SCC is increased when cement is replaced with metakaolin and RHA, as the flow resistance of the blended cement increases due to the increase in the water demand of the system [31].

2. Research gap

Previous studies have investigated the suitability of multi-blend of CC and RHA for the production of the SCC as reviewed by [20]. Most researchers focused on the use of metakaolin as CC, which is an expensive material due to its frequent use in other competing industries and is less available compared to low-kaolinitic CC [23,24]. There is lack of knowledge when it comes to the use of low-kaolinic CC as a sole SCM or in combination with RHA as a partial replacement to cement in SCC as pointed out by [20]. More so, previous studies have investigated the effects of blends of metakaolin and RHA on the SCC fresh properties, strength, and durability. However, the effects of these materials on the rheological properties of SCC in terms of yield stress, plastic viscosity, shear thickening behaviour, workability retention, plastic shrinkage, and drying shrinkage have not been reported [20]. Therefore, current efforts are aimed at optimizing the SCC mix design using a multi-blend of low-kaolinic CC and RHA as a partial replacement for cement. Other properties to be investigated include the rheology, time-dependent workability, evolution of hydrate phases of the binder, plastic and drying shrinkage, compressive strength, and rapid chloride migration.

3. Materials and methods

3.1. Research materials

Self-compacting paste, mortar and concrete are produced using CEM I 42.5 R conforming to DIN EN 197-1 [9]. According to the supplier, the cement contained the mineralogical phases (wt-%) 61.6 C₃S, 18.2 C₂S, 5.8 C₃A, 9.0 C₄AF, 0.6 calcite and 3.2 sulfates. The cement is partially replaced by 15 vol-% LP to form a Portland limestone cement (PLC). The LP contained 99.8 wt-% calcite and 0.2 wt-% quartz. The PLC is partially substituted with the binary blends of CC up to 40 vol-%, binary blends of RHA up to 40 vol-% and the ternary blends of CC and RHA up to 40 vol-% to determine the influence of CC and RHA on the rheological properties of SCC. The raw material for CC is an Amaltheen clay from southern Germany, which was calcined on an industrial scale at 750 °C and ground with an industrial roller mill to the fineness described in Table 1. The CC contained (wt-%) 60.8 amorphous phase, 2.2 muscovite, 16.2 quartz, 4.6 illite, 0.6 calcite and 1.6 sulfates mineralogical phases as characterized previously by [32]. For the RHA, rice husks from the vicinity of Zaria in Kaduna State, Nigeria, were calcined at 650 °C for 2 hours in an electric furnace and ground with a laboratory scale mill to obtain the RHA. It contained 96.8 % wt-% amorph silica as the mineral phase, measured using an internal standard. Table 1 shows the physical properties of the research binders. The particle shape of CC and RHA was examined using Evo LS 15 (Zeiss, Germany) scanning electron microscope (SEM). Both CC and RHA were scattered on a thin adhesive layer and coated with gold before SEM images were taken.

The fluidity of the SCC is controlled with the use of superplasticizer (SP) which has a total solid content of 38.6 wt-%, 1390 micromoles/g anionic charge density, 25992 g/mol molecular weight and a side chain length of n_EO = 31 according to the supplier’s information. To complete the SCC mix design, sand with a grading 0/4 mm, a particle density of 2.87 g/cm³ and having 7.6 wt.% passing sieves 0.125 mm was used as fine aggregate (FA). While round gravels with a grading 4/16 mm, a particle density of 2.68 g/cm³ and 2.7 wt-% passing sieves 0.125 was used as coarse aggregate (CA). Figure 1 shows the particle size distribution of the fine and coarse the aggregates used.

3.2. Methods

3.2.1. Self-compacting paste, mortar and concrete rheological assessment

The powder type of SCC used for the study was designed using a stepwise empirical method. This implies designing the paste phase of the concrete first. The amount of water confined by the binder is determined using the spread flow method. At a constant volume of the powder, the volumetric water-to-powder ratio (V_w/V_p) is varied between 1 to 2 at 0.1 intervals. Four points were used for each binder system, and the relative spread is determined using Equation (1). The V_w/V_p is plotted against the relative spread, and the amount of water confined by individual binder system (V_wΓo) is determined by extrapolating the points to the vertical axis [5].

Γ_RS = [d/d_o]² - 1

(1)

Where Γ_RS = relative spread area, d = (d₁ + d₂)/2, d₁ = largest flow diameter and d₂ = diameter perpendicular to d₁, and d_o = diameter of mini-slump cone, 100mm.

The influence of CC and RHA on the amount of water confined by the PLC was determined and was used as the basis for establishing the V_w/V_p of the self-compacting paste systems (SC-P) using Equation (2).

V_w/V_p = [0.8 to 0.9] ∙ V_wΓo

(2)

where V_wΓo = volume of water confined by binder in relation to its volume

The amount of the SP required to deform the SC-P systems was determined as the dosage of SP at which a particular binder system attained a flow diameter of 240 mm ± 20 mm. Self-compacting mortar (SC-M) design was achieved by considering the average V_w/V_p required to deform SC-P, and the volume of the fine aggregate (V_s) is fixed at 44 vol-% of the SC-M volume. The amount of SP is adjusted until for the individual SC-M systems self-compactability is attained. The deformability of the SC-M systems was assessed by measuring the slump flow using the mini-slump cone [5] and the range of 240 mm to 260 mm was used as a yardstick for indicating the deformability limit at which self-compactability is achieved. The viscosity of SC-M was monitored by measuring the mini V-funnel time [36], while visual inspection was used to evaluate the segregation resistance of the SC-M. To complete the SCC mix design, the volume of the coarse aggregate is adjusted together with varying the dosages of the SP until it was kept at 33 % of the total SCC volume. The air content was also fixed at 2 vol.% of total SCC volume, according to (Efnarc, 2002).

SC-P mixes were produced according to DIN EN 196-1 [37]. The binder, mixing water and the SP were added together and mixed for 4 minutes in a mortar mixer produced by Bluhm and Feuerherdt GmbH, Berlin, Germany. SC-M was produced by mixing the constituents for 8 minutes in the same mixer described above. The binder materials, FA and two-third of the mixing water were mixed for 2 minutes, followed by a break of 1 minute to enable the addition of the remaining water and the SP. The entire mixture was then mixed for an additional 5 minutes. The mixing sequence of SCC started with mixing the binder, FA, and CA for 1 minute in a UEZ ZM 50 concrete mixer (UEZ-MISCHTECHNIK), with the capacity of 60 liters and the mixing speed of 48 rpm. Two-thirds of the mixing water was then added while the mixer was running and mixed for 2 minutes. The SP and the remaining mixing water were then added and the whole constituents mix for another 7 minutes.

The deformability of the SCC in absence of obstacles was evaluated using the slump flow according to [27] while the J-ring test was employed to assess the passing ability the SCC through an obstacle according to [29]. The viscosity of the SCC systems was assessed using both the T₅₀₀ time and the V-funnel test according to [28]. The stability of the SCC was evaluated in two ways. First, using the sieve stability assessment method according to [38] and the washing test according to [39] where the fresh SCC was poured in to a plastic cylinder 150 x 500 mm (with a solid base and cut at third points up to half of the circumference to accommodate metal dividers). The cut points for receiving the metal dividers were sealed with an adhesive tape before pouring the SCC. Immediately after mixing, the SCC was poured into the cylinder and stored vibration-free for 30 minutes until the time of testing. After 30 minutes, the adhesive tape is removed and the metal dividers are inserted. The SCC is then poured into vessels in segments and washed through 4 mm aperture sieve. The sieve residue was dried in a ventilated oven at 105 °C and weighed.

The uniform distribution of the CA in the SCC mixtures is monitored over time using a plunger method [30]. SCC is poured into a hollow cylinder with an internal diameter of 150 mm and a height of 600 mm. A 900 g steel plunger with a diameter of 14 mm and a height of 750 mm is then guided through the guide tube (with 3 openings) to the surface of the SCC and released to penetrates into the SCC. The depth of immersion of the steel plunger is measured and the sedimentation height (h_s) is calculated as the difference between the steel plunger height (h₀) and the immersion depth (h_T) in mm. the steel plunger and the guide tube are withdrawn, cleaned and dried for the next measurement. Previous immersion holes were avoided by changing the position of the guide tube after the whole available guide holes have been exhausted.

Rheology of the SCC in terms of the shear stress (τ), plastic viscosity (µ) and flow resistance (F_R) were determined using a rotational rheometer, viskomat XL (Schleibinger Geräte) with a vane probe testing paddle at a constant temperature of 20 °C. The measurement started with the maximum rotational speed of 12 rpm for 80 s and decreased in 14 steps of 20 s each until the end of the measurement [40]. The recorded torque were used to estimate the yield stress (τ₀) and plastic viscosity (η) of the SCC according to the Bingham model [41,42] using Equation (3). The workability retention of the SCC is monitored by calculating F_R of the SCC mixtures over time (area under curve) obtained by plotting the torque against the velocity as described previously by [31].

$$T=g+N\bullet h$$

(3)

where T = torque ≈ τ; g = y-intercept of the flow curve ≈ τ₀; N = velocity ≈ γ˙; and h = the slope of the curve ≈ η.

3.2.2. Plastic and mechanical properties of self-compacting paste, mortar and concrete

The plastic shrinkage of SC-M at an early age was measured contactless using a shrinkage cone (Schleibinger Testing Systems, Buchbach, Germany) according to [43]. The measurement was started 15 minutes after water addition and lasted for up to 48 h. Polypropylene foil was used to prevent the friction effect between the fresh SCC surface and the shrinkage cone. The SC-M drying shrinkage was measured on 40 × 40 × 160 mm³ prisms according to [44].

The portlandite (CH) consumption by the CC and RHA and hydrate phases formed at 2, 7 and 28 days of curing were investigated by thermogravimetric measurements (TG) conducted in Netzsch STA 449 F3 Jupiter apparatus. The constituents of the SC-P were mixed according to [37] and filled into 40 × 40 × 160 mm³ steel molds and stored moist for 48 h and then cured under water until testing. At the age of testing, a representative portion of the sample is manually chipped out from the inner part of the prisms and crushed to < 1 mm size using the laboratory pestle and mortar. Hydration of the pulverized binder was stopped by solvent exchange as described in [45]. Approximately 300 mg of the pulverized binder was placed in alumina crucibles and heated to 1000 °C at a heating rate of 2 °C/min under a nitrogen atmosphere. The bound water was determined as weight loss (wt-%) from the TG measurements between 25 °C and 400 °C, while the CH content was quantified by the tangent method from the weight loss between 400 °C and 490 °C.

For the compressive strength measurement, SCC was cast into 150 × 150 × 150 mm³ steel molds and stored moist for 48 h and then cured underwater until the test date. The measurement was conducted according to [46] at 2, 7 and 28 days of curing on the Form + Test Prüfsysteme Alpha 1-3000 strength testing equipment with an increasing uniform loading rate of 2400±200 N/s until failure. The influence of CC and RHA on chloride resistance of SCC was investigated using a rapid chloride migration by applying an electric field axially to the test specimen to accelerate the chloride penetration, according to [47]. The depth of chloride penetration was determined on 100 x 50 mm³ cores drilled and subsequently sliced from 150 × 150 × 150 mm³ SCC specimens at the age of 28 days of curing.

4. Results and discussion

4.1. Optimization of SCC mix design with the blend of CC and RHA

To optimize the blend of CC and RHA as partial replacement to PLC in SCC, the influence of CC and RHA on the amount of water confined by the binder was first considered. PLC without CC and RHA partial replacement confined approximately a volume of water equal to the volume of solid. A substitution by 10 vol-% CC showed no significant effect on the volume of water confined and increased to 11 vol-% of water at substitution ratio of 40 vol-%. RHA at 10 vol-% PLC substitution confined 20 vol-% additional water compared to the PLC, and the volume of water confined increased to 43 vol-% at RHA substitution ratio of 40 vol-%. Figure 2 shows the V_w/V_p for CC, RHA and the ternary blends of CC and RHA.

However, the ternary blends of CC and RHA yielded no any reduction in the V_wΓo due to the high-water demand of RHA, for instance, the V_wΓo for 40 vol-% CC replacement is 1.15 and increased drastically to 1.37 when 5 vol-% of CC is replaced by RHA in the blend (35CC,5RHA). Figure 2 shows the relationship between the water demand and the ratio of confined water by the binder systems. The ternary blends of CC and RHA appeared above the line of best fit, while the binary blends appeared on the line or below.

A possible explanation for this behavior of the ternary blends is the dominating influence of RHA on the properties of the blended binder. Even a small amount of RHA in the ternary blend leads to an increase in both, the water demand and the amount of water trapped by the binder compared to the binary CC mixes. It could also be due to improper mixing of the two materials, since CC has a heterogeneous surface morphology, while RHA contains an irregular, granular surface of isolated plate morphology as shown in Figure 4, so the presence of CC in the mixture does not have a significant effect on reducing the water demand of ternary mixtures.

The design of SCC starts with the determination of the V_w/V_p required to impart on paste self-compactability. This V_w/V_p is calculated from the volume of water confined by the individual binder system, and the average of these values for the individual binder systems are shown in Table 2. PLC requires an average of 0.87 V_w/V_p to achieve self-compactability. Partial substitution of CC up to 20 vol-% has minor effect on this value, CC partial substitution beyond 20 vol-% requires an adjustment of this value or an increase of the SP dosage to achieve similar deformability class as the PLC system, as previous investigation by [48] achieved self-compactability using the same V_w/V_p and increasing SP dosage, with up to 40 vol-% CC in SC-M. On the other hand, the partial substitution of PLC with RHA requires an significant increase of V_w/V_p to achieve self-compactability. At 10 vol-% RHA partial replacement, V_w/V_p already increased to 1.1, which is 21 % higher than the value required for PLC. At 40 vol-% RHA partial replacement, the V_w/V_p increased by 42 %. In this case, the SP adjustment is not sufficient to achieve the required degree of deformability because of the higher water demand and specific surface area of the RHA compared to PLC. Therefore, urgent adjustment of the V_w/V_p of the RHA and the ternary blend of CC and RHA systems is required to achieve a deformability characteristic similar to that of PLC.

The SCP design in this section will later be used as a binder in SC-M and SCC. Therefore, the selection of the V_w/V_p will be done considering the intended final use of SCC. The following outlook is considered to justify the selection of V_w/V_p for the SCP design. In practice, the water-to-binder (w/b) and the strength of the binder determined the strength and durability class of the concrete and thus its application [49,50]. To achieve SCC with PLC, a V_w/V_p = 0.87 is required, corresponding to a w/p = 0.29; for CC replacement up to 40 vol-%, a w/p = 0.32 is required. For 10 vol-% RHA, w/p = 0.36 is required, increasing to 0.42, 0.45, and 0.50 for 20, 30, and 40 vol-% partial replacement, respectively. [51] achieved self-compactability using a w/b = 0.26 with up to 20 wt-% RHA as partial replacement for cement in SC-M, and despite increasing dosages of SP, RHA increased the viscosity of the SC-M. It should be noted at this point that the deformability of the SC-M doesn’t necessarily indicate the deformability of SCC, because SCC contains a large volume of coarser aggregate in addition to SC-M, which has a significant impact on its deformability characteristics. [52] achieved self-compactability using a low w/p = 0.28 and the same dosage of high range water reducers with RHA substation up to 20 wt-%, but the viscosity of 20 wt-% RHA binary blended SCC was 63 % higher than the control (viscosity = V-funnel time). The same deformability characteristic as the reference systems with higher RHA replacement ratios (≥ 20 wt-%) were achieved by increasing the w/p to 0.44 and above [53,54,55]. Another factor that governs the selection of the w/b is the expected performance of the SCC after hardening. For chloride exposure under alternating wet and dry conditions, the maximum allowable w/b is 0.45 [49].

Partial replacement of PLC with CC even up to 40 vol-% yields the required deformability characteristics and has a wide applicability in different durability exposure classes, as previously reported by [48,56] while providing significant savings of production cost and reducing CO₂ emission. Higher PLC partial substitution with RHA up to 40 vol-% is also possible using a higher w/p of ≥ 0.5, this concrete could also have a wide range of applications, for instance in exposure classes X0, XC, and some classes of XD and XS exposure according to [49]. Considering that RHA poses a challenge to deformability at higher PLC partial substitution due to its high-water demand, this study will limit the RHA replacement ration to 20 vol-%. For comparison, the binary blend with CC will also be kept at 20 vol-%, and the ternary blend will use 10 vol-%CC + 10 vol-%RHA. Therefore, V_w/V_p = 1.275 required to impart self-compactability to the 20 vol-% RHA binder system is considered as the V_w/V_p in the following and is used to established the SP dosages required to deform the SCP systems, as depicted in Figure 5.

Based on the visual inspection, SC-P achieved deformability without segregation at a flow diameter of 220 to 265 mm. Therefore, the dosage of SP is established which is necessary for the individual binder systems to achieve a flow diameter 240 mm ± 20 and without segregation. The latter is assessed visually. PLC binder system (SC-P) requires an SP dosage of between 0.05 to 0.1 wt-% to achieve self-compactability. SC-P-20CC demands a slightly higher SP dosage as SC-P, while for the SC-P-20RHA system, the SP dosage already increases drastically to 0.3 wt-%, although this is reduced to 0.25 with the SC-P-10CC+10RHA blend. The increase in the SP demand is due to the higher water demand of RHA, which continues to trap water in its structure and requires more SP to achieve the required degree deformability. The final SCP mix design is shown in Table 3 and were used as basis for SC-M design and to measure the portlandite over the period of 28 days of curing.

The SCP designed above were used in the next step as media to deform the SC-M and bind the fine aggregate. The SC-M mix designs are achieved by fixing the volume of the fine aggregate (V_s) at 44 vol-% of the total SC-M volume, based on the recommendation of (EFNARC 2002). SP dosages are adjusted to achieve the required degree of deformability. Figure 6 shows the deformability and the rate of deformability of the individual SC-M systems.

With a slight adjustment of the SP dosage, SC-M-1-20CC achieved a similar deformability to SC-M-1, SC-M-1-20RHA and the blend SC-M-1-10CC+10RHA could achieved a similar deformability class to SC-M-1 but with an increased viscosity and higher SP dosages. For deformability assessment, (EFNARC 2002) guidelines were adopted. A range of 240 mm to 260 mm flow diameter and a viscosity class (V-funnel time) of 7 s to 11 s were used. Only SC-M-20RHA falls under these limits. The remaining mixtures exhibited a higher flow rate, indicating low viscosity. Therefore, mixtures that are stable (judged by visual assessment) between the flow diameter = 240 mm to 260 mm were considered for the production of the SC-M specimens. Table 4 provides the final SC-M mix designs which were used to monitor the influence of CC and RHA on plastic and dry shrinkage strains.

The final SCC mix design is achieved with a fixed CA content of 33 vol-% and assuming an air content (V_a) of 2 vol-% of the total SCC volume according to (EFNARC 2002), while the SC-M designed above complete the remaining SCC volume. The SP dosages were adjusted until an acceptable deformability is achieved as shown in Figure 7(a). Criteria for assessing the deformability of SCC in the absence of obstacles (filling ability) include the slump-flow, V-funnel and t₅₀₀ times as an indication of viscosity, while the use of J-ring can give an estimation of the deformability in the presence of obstacle (passing ability). The combination of these assessments was used as the basis for the selecting the appropriate mixes to produce the final SCC. By adjusting the SP dosages, SCC-1 achieved a deformability class SF2 and viscosity class VS1 and VF1 according to [50]. With a slight increase in the SP dosage, SCC-1-20CC achieved similar deformability to the SCC-1, with viscosity classes of VS2 and VF1. SCC-1-20RHA exhibited higher viscosity than SCC-1 and requires an increased SP dosage to attain deformability class SF2 and viscosity classes VS2 and VF1. The ternary blended, SCC-1-10CC+10RHA, exhibited a deformability and viscosity behavior somewhat in-between that of binary CC and RHA SCC. The increased viscosity with RHA substitution is due to the higher water demand of RHA compared to PLC and CC as depicted in Table 1. A relationship between the V-funnel time (VF) and the t₅₀₀ (VS) measured together with the slump-flow is observed with a high correlation [57] as shown in Figure 7 (b).

Similarly, by adjusting the SP dosages, the blocking tendency of the SCC decreases and its possible to bring all the SCC mixtures to a passing ability class PJ2, classified according to [50] (Figure 8).

The reference mixture (SCC-1) exhibits with an SP dosage of 0.3 good passing ability, but the viscosity (V-funnel time) falls below 6 s, the minimum recommended by (EFNARC 2002) (Figure 7 (b)). The tendency of segregation is high with this mixture, and therefore it was not considered for the production of final SCC. The viscosity of the SCC depends largely on the w/p: The higher the w/p the higher the rate at which the SCC will flow, as previous investigations obtained VF time ≤ 6 s using w/p ≥ 0.5 [4,58]. When the w/p is < 0.4, SCC have a VF time ≥ 6 s [53,56]. SCC-1 with 0.25 SP dosage is at the limit for both the filling and passing ability values, but is considered suitable for the final SCC mix design. The selection criterion for the final SCC mix design is therefore based on SF ≥ 650 mm, VF ≥ 6 s and PJ ≤ 10 mm and the proportions of the final SCC mix designations are presented in Table 5 and Table 6, and are used to determine the influence of CC and RHA on the segregation resistance, rheology, time dependent workability, compressive strength and chloride migration resistance of SCC.

The reference system (SCC-1) required a V_w/V_p = 0.87, corresponding to w/p = 0.29, for self-compactability, similar to that previously used by [48,52] to achieve high-strength SCC. Both CC and RHA have a water demand greater than that of PLC, the water demand of CC is one third higher than that of PLC (see Table 1) but required only an adjustment of SP to achieve a degree of deformability comparable to SCC-1, although with an increased viscosity and SP demand as previously investigated by [48,59]. The increase in viscosity is not only due to the higher water demand of the CC compared to PLC but also due to its different particle shape [31,60] leading to an increased resistance to flow and hence higher SP demand to deform the SCC-1-20CC system. The use of RHA as partial replacement to PLC in SCC is more critical due to its more than three time high water demand (see Table 1). Unlike the SCC-1-20CC system, SP adjustment is not sufficient to deform SCC-1-20RHA and even the SCC-1-10CC+10RHA system. Therefore, V_w/V_p adjustment is urgently needed to achieve self-compactability. When substituting high proportion of PLC with RHA (20 % and above), higher w/p, from 0.44 and above will be required to properly deformed the RHA-SCC system. This affects the concrete porosity and limits its applications [49]. Therefore, this study limits the content of RHA to 20 vol-% and uses a Vw/Vp = 1.275 (0.42 w/p equivalent) for all PLC-, CC-, and RHA-SCC systems.

4.2. Influence of CC and RHA on the segregation resistance of SCC

Both, short-term and time dependent segregation resistance assessments are conducted to established the influence of CC and RHA on the stability of the SCC. For the short-term assessment of segregation resistance, sieve stability and washing tested are conducted after the fresh SCC has settled 30 minutes after mixing. Figure 8 (a) shows the segregated portion of the SCC specimens determined by sieve stability. The segregated portion of all the SCC specimens is less than 11 wt-%, which is within the limit specified by [50].

The proportions of the coarse aggregate from the three segments of the cross-section of the fresh SCC evaluated by aggregate washing test are shown in Figure 8 (b). The mass deviation of the coarse aggregates from the three segments of all the four test specimens is less than 4 wt-% and thus significantly below the limit (15 wt-%) specified in [39].

The stability SCC specimens is monitored for the first 90 minutes by sedimentation analysis using a plunger method. SCC-1 and SCC-1-20CC remain stable until 75 minutes indicated by the plunger almost reaching the bottom of the cylinder. At 90 minutes the immersion depths decrease indicating that setting has started. SCC-1-20RHA and the ternary blend SCC-10CC+10RHA also showed similar sedimentation tendencies. In this case, the stability retention lasts up to 30 minutes beyond which the plunger only sinks to the halfway down the cylinder and at 60 minutes the penetration is virtually not possible due to the stiffening of the SCC surface (Figure 10).

The short-term stability of all SCC mixes is within the specified limits [39,50] and even SCC-1-20RHA retains its workability up to 30 min after mixing. While for the time dependent workability assessment, the use of RHA as partial replacement to PLC is considered critical because the mixing water was absorbed after 30 min of mixing, making the mix stiffer and rapidly losing its self-compactability. The time dependent stability assessment using plunger method assumed the free sinking of the plunger down to the bottom of the concrete anytime it was guided until setting and hardening occur, which is about 90 min depending on the type of cement used [30]. Excessive settlement of the coarser aggregate during the early time of the SCC are considered to hinder the sinking of the plunger, signifying segregation had occurred. In this regards, SCC-1 and SCC-1-20CC behaved apparently stable and maintained their stability until 75 min after mixing. For SCC-1-20RHA and SCC-1-10CC+10RHA, a rapid loss of stability was observed after 30 min of mixing, which is attributed to the continued suction of the mixing water by RHA and not to the settlement of the coarse aggregate, since the hardened SCC with RHA as PLC partial replacement still exhibited a uniform distribution of the coarse aggregate across its section, as shown in Figure 11 (c) and (d).

Segregation resistance is an important attribute that determines the acceptability of SCC. It can be measured by sieve stability, which measures the bleeding of SCC after 30 min of resting. The SCC-1 system has a sieve stability value similar to what was obtained by [61], and all the SCC systems meet the requirements of [50] for segregation resistance acceptance. The wash test was also used to measure the uniform distribution of the coarse aggregate over the fresh SCC section after 30 minutes of settlement, and all SCC specimens retained the coarse aggregate in suspension during the test period. The only stability issue observed is the stiffening of the RHA-SCC systems, which is critical after 30 min of production due to the continues suction of the mixing water by RHA, which may limit applications where longer retention of workability is required.

4.3. Rheological and time dependent workability retention of SCC

The time-dependent rheological assessment of SCC begins with determining the influence of CC and RHA on the torque required to initiate and maintain displacement of SCC based on the applied shear rate measured with a viscometer as depicted in Figure 12. At 15 min of testing, SCC-1 recorded a torque of 66 Nmm at a lower velocity of 1 rpm, and 109 Nmm at the maximum applied velocity of 12 rpm. After 90 min of testing, the torque increased to 133 and 228 Nmm, respectively. SCC-1-20CC required lower torque to achieve and maintained displacement compared to SCC-1, both at lower and higher velocities and at all test times. Although CC has a higher water demand than PLC, the decreased torque could be due to the higher dosage of SP applied to deform the SCC-1-20CC system, despite both binder systems required almost similar V_w/V_p to achieve self-compactability as shown in Table 2. For the RHA binder system, on the other hand, at 15 min of testing, a torque of 102 Nmm was measured at lower velocity and 180 Nmm at higher velocity. These values increased significantly after 30 min of testing due to the stiffening of the SCC-1-20RHA mixture as a result of higher water demand of RHA (see Figure 10). The ternary blend with CC and RHA behaved somewhat in between the SCC-1-20CC and SCC-1-20RHA, the presence of the CC in the blend decreased the torque required to achieve displacement at 90 min of testing by 53 and 59 % at lower and higher velocities, respectively, compared to RHA-SCC system.

Establishing the dynamic yield stress of SCC is important to determine the extent of energy required to maintain SCC flow; this is important to ensure uniform deformability of SCC across formwork sections. The time-dependent yield stress and plastic viscosity of SCC were established from the measured torque values induced by the applied velocity using a Bingham model as presented in Figure 13. SCC-1 has a yield stress of 60 Nmm and a plastic viscosity of 3.9 Nmm*min at 15 min of testing, which gradually increased to 120 Nmm and 8.2 Nmm*min, respectively, after 90 min of testing. SCC-1-20CC showed a similar increasing tendency in yield and viscosity values as SCC-1. The gradual increase of the yield stress and plastic viscosity could be due to the loss of water from the surfaces of SCC caused by evaporation, or due to the chemical reaction between the binder and mixing water leading to the initial formation of ettringite [62]. SCC-1-20RHA had a yield stress of 88.5 Nmm and a plastic viscosity of 6.2 at 15 min of testing, which are 47 and 59 % higher than SCC-1, respectively. This yield stress and plastic viscosity values increased rapidly up to the 90 min of testing unlike the SCC-1 and SCC-1-20CC systems. The rapid increase of both yield stress and plastic viscosity values is due to the increase plastic stiffening caused by the continues absorption of the mixing water by the RHA particles. The ternary blend of CC and RHA had both, lower dynamic yield, plastic viscosity values and smaller rate at which they increased compared to SCC-1-20RHA. In all cases, SCC mixtures containing RHA exhibited higher yield stress and plastic viscosity values, due to their higher water demand.

The workability retention of SCC is monitored by comparing the flow resistance of the SCC mixes over a period of 90 minutes. The flow resistance is determined as the area under the curve of the torque plotted against the velocity values from Figure 12. The flow resistance of SCC-1 measured 15 min after water addition is 933 Nmm/min and increases to 1900 Nmm/min after 90 min (Figure 14). SCC-1-20CC mixture exhibits similar flow resistance to SCC-1 up to 90 min of testing. SCC-1-20RHA, on the other hand, had a flow resistance value of 1388 Nmm/min at 15 min, which is 30 % higher than SCC-1 and increased to 8205 Nmm/min at 90 min of testing. SCC-1-10CC+10RHA showed similar flow resistance to SCC-1-20RHA up to 30 min of testing, after which it increased less compared to SCC-1-20RHA. The decrease in flow resistance of SCC-1-10CC+10RHA is due to the presence of CC in the blend, which reduces the water demand and SSA of the system.

Generally, by increasing the SP dosage, PLC partial replacement with 20 vol-% CC has no effect on time dependent workability retention of SCC up to 90 min and therefore, SCC-1-20CC can be used to produce both in-situ, precast and ready-mix SCC. However, the use of 20 vol-% RHA and the ternary blend 10CC+10RHA developed high flow resistance and exhibited rapid loss of workability after 30 min of mixing. Therefore, their workability retention needs to be improved for applications beyond 30 minutes.

The relationship between the flow resistance time-dependent workability measurement and the sedimentation analysis conducted by plunger method is valid in the case of SCC-1 and SCC-1-20CC up to 75 min of testing, while for the SCC-1-20RHA and SCC-1-10CC+10RHA, the relationship is valid only up to 30 min of testing (Figure 15). The penetration of the plunger is not possible in the SCC mixes containing RHA after 45 min of testing due to the stiffening of SCC surface which hinders the plunger penetration.

The differences between the two methods of time-dependent workability assessment could be explained from the mechanism of time-dependent workability loss due to structural build up (thixotropy), that can easily be reversed during the viscometer rotation in the flow resistance assessment method, while for the sedimentation analysis, the plunger is only guided and allowed to penetrate the concrete on its own weight, the SCC remained undisturbed and structural build ups unreversed.

4.4. Formation of hydrate phases from the hardened SCP

The formation of SCP hydrates phases was determined at 2, 7 and 28 days of hydration (Figure 16). The mass loss between 50 °C to 140 °C is due to dehydration of the ettringite (E) and calcium silicate hydrates (C-S-H) [63] and increases with an increase in the hydration time for all the SCP specimens. The second mass loss is observed between 140 °C and 190 °C due to the dehydration of the monophases (AFm) [64] and is more pronounced in the SCP with RHA partial replacement in all hydration stages. Portlandite decomposition occurs between 400 °C to 450 °C for all SCP specimens, while calcium carbonate (CaCO₃) decomposition takes place between 600 °C to 800 °C (Figure 16). The pattern of the formation of the hydrate phases is similar to was observed previously by [48] when CC was used as partial replacement to PLC in SC-P.

The partial replacement of PLC by CC and RHA has a noticeable effect on the formation of hydrate phases, especially in the ranges of mass loss between 140 °C and 190 °C and between 400 °C and 450 °C. At 2 days of hydration, the DTA peak due to the dehydration of carbonate AFm phases is not evident in the SC-P and SC-P-20CC systems by TG measurements due to the increase of the Vw/Vp ratio used in this study, as the previous study by [48] noticed the formation of these phases in SC-P and SC-P-CC systems at the same age of hydration using a V_w/V_p = 0.875. The reaction between the LP and CC enhanced the formation of the carbonate AFm phases at 7 and 28 days of hydration. This increased the volume of the hydration products in the SCP-CC system and densified its microstructure, as previously reported by [48]. RHA and the ternary blend of CC and RHA enhanced the precipitation of theses phases even at 2 days of hydration and continue to increase up to 28 days of hydration.

Figure 17 shows the influence of CC and RHA on the portlandite (CH) consumption. SC-P has the highest CH content at each test age, while SC-P-20RHA exhibits the lowest CH content. SC-P had a CH content of 9.4 g at 2 days, 12.3 g at 7days and 14 g at 28 days. The CH content of SC-P-20CC at 2 days 7.9 g and increased to 10.2 g and 10.6 g at 7 and 28 days, respectively. SC-P-20RHA had a CH content of 5.8 g at 2 days, which increased to 6.8 g at 7 days and decreased to 5.8 g at 28 days. The CH content of SC-P-10CC+10RHA is half way-between that of SC-P-20CC and SC-P-20RHA at all test ages.

The CH content of SC-P increases over the experimental period due to the continued hydration of C₃S and C₂S in the clinker portion of PLC. The use of CC and RHA as SCM reduced at 2 days of hydration the CH content, mainly due to the dilution effect. Simultaneously, CC and RHA provide more nucleation sites for precipitation of hydration products at this stage of hydration, as previously observed by [48,65]. The relative decrease in CH content at 7 days of hydration is due to the dilution effect and the initiation of the pozzolanic reaction of CC and RHA, which consumes CH. At 28 days of hydration, CH consumption is significant, especially in SCPs with RHA as a partial substitute for PLC. This is indeed expected and attributed to the pozzolanic effect of CC and RHA, which consumed the CH and produced more C-S-H, which densified the SCP microstructure and thus increased the strength of the SCC, as can be seen later in Figure 20.

4.5. Plastic and hardened properties of self-compacting mortar and concrete

4.5.1. Effect of CC and RHA on plastic and total shrinkage of self-compacting mortar

The mechanism of SC-M shrinkage during the early age of hydration can be explained in three stages. First, plastic shrinkage, during the very early hydration phase, from water addition to about 7 h. The SC-M experiences a transition from fluid to a plastic material. During this period, the rate of plastic shrinkage of SC-M-1 and SC-M-1-20CC is high, reaching up to -7.0 mm/m (Figure 18). This value is somewhat lower to -5.2 and -6.5 mm/m in SC-M-1-20RHA and SC-M-1-10CC+10RHA, respectively. This high plastic shrinkage values of SC-M at this stage is due to the particles settlement caused by gravity leading to an increased packing density of the SC-M, and forcing the free water to rise to the surface of the SC-M, resulting to bleeding [66] and evaporation of moisture from the surfaces of the SC-M leading to the formation of water menisci, which eventually create a negative capillary pressure that contracts the SC-M particles and consequently causes volumetric contraction [67,68]. It has been reported that the use of shrinkage reducing admixtures (SRA) reduced the plastic shrinkage of SCC at this stage of hydration by reducing the internal friction angle between SCC particles due to their high fluidity and delaying the setting time of SCC [66]. RHA is expected to behave similar to the SRA in reducing the plastic shrinkage of the SC-M because it delays the initial setting time of the blended cement [69]. The second stage last from 7 to 16 h after water addition. Here, the plastic shrinkage rate of SC-M-1 decreases and yields a shrinkage value of -7.3 mm/m, while SC-M-20CC exhibits no further plastic shrinkage. Plastic shrinkage increases for the two other SC-M yielding -5.5 mm/m for SC-M-20RHA and -6.6 mm/m for SC-M-10CC+10RHA. Finally, after 16 h of hydration, the plastic shrinkage remains constant until the end of the measurement. The reason for the plastic shrinkage of the SC-M beyond 7 h of hydration could be due to the continuous evaporation of moisture from the SC-M surfaces, volume reduction due to water consumption by the hydration process, as previously observed by [48,67,68] In general, the reduction in plastic shrinkage after 7 h of hydration due to the partial replacement of CC and RHA in SC-M could be attributed to the fact that both act as nuclei for the formation hydration products at an early age of hydration, thereby increasing the volume of hydration product and densify the SC-M microstructure [70]. And for the RHA and ternary blend of CC and RHA, the reduction in plastic shrinkage could also be due to the release of the early absorbed water by the RHA particles, thereby increasing the internal relative humidity of the SC-M and reducing the autogenous shrinkage at an early age of the SC-M [71].

The effect of partial replacement of PLC with CC and RHA on the total shrinkage of SC-M was measured on 40 × 40 × 160 mm³ prisms as presented in Figure 19. SC-M-1 and SC-M-1-20CC exhibited the same drying shrinkage values at all test ages up to 14 days, after which SC-M-1-20CC shrank less than SC-M-1. SC-M-1-20RHA has the highest initial drying shrinkage of all SC-M specimens until about 14 days when it decreased yielding shrinkage values similar to SC-M-1 at 56 days. From 21 days and beyond, SC-M-1-10CC+10RHA shrank more than the other specimens.

The total shrinkage of SC-M specimens is a combination of drying shrinkage caused by the continuous loss of water from the capillary pores of the SC-M to equilibrate the relative humidity of the surrounding environment and autogenous shrinkage due to the reduction of water by the hydration process. SC-M-1 and SC-M-1-20CC have the same total shrinkage tendency up to 28 day of testing, beyond 28 day of testing, CC decreased the total shrinkage of the SC-M partly due to the volume increase of hydration product from the formation of more carboaluminate AFm phases, as shown previously in Figure 16, and or due to lower amount of evaporable water because by the pozzolanic reaction of the CC, which consumes more water, as previously reported by [72] in the case of using metakaolin as partial replacement for cement. RHA and the ternary blend of CC and RHA in SC-M specimens exhibit a different pattern of total shrinkage, RHA-SC-M specimens shrank more than other specimens up to 7 days of testing due rapid evaporation of the absorbed water from the surfaces of the RHA-SC-M specimens, as the absorbed water was reported by [73] as having higher mobility than the water in the capillary pores and could evaporate easily, and thus an increase of the drying shrinkage. Beyond 7 days of testing, the total shrinkage of RHA-SC-M decreased and equal to that of PLC-SC-M from 56 days and 91 days. The improvement of the total shrinkage could be due to further release of absorbed water by RHA to restrain the decrease of the internal relative humidity of SC-M and thus a decrease of the total shrinkage. This phenomenon was explained previously by [71] when RHA was used as an internal curing agent in cement paste. From 21 days of testing and beyond, SC-M-1-10CC+10RHA shrank more than any other specimen due to continues evaporation of the absorbed water from its surfaces.

4.5.2. Compressive strength and rapid chloride migration assessment of SCC

The impact of the CC and RHA on the development of compressive strength of SCC up to 28 days is shown in Figure 20. SCC-1 achieved higher values of compressive strength at 2 and 7 days. All the remaining specimens exhibited similar compressive strength values at 2 and 7 days, which are 8 % and 21 % lower than SCC-1, respectively. At this stage of curing, CC and RHA behaved similar and their physical presence resulted in a dilution effect and thus a reduction of the compressive strength, as observed previously by [48] when CC was used as a partial replacement to PLC in SC-M. At 28 days, SCC-1 and SCC-1-20CC reach similar compressive strength values while a slight increase of 6 % is observed compared to SCC-1 for SCC-1-20RHA and SCC-1-10CC+10RHA due to the pozzolanic reactive of CC and RHA. The use of RHA and the blend of CC and RHA at 28 days of curing behaved similar to silica fume in improving the compressive strength of SCC beyond the level of the pure cement as previously observed by [74,75]. Another explanation to the increase of the compressive strength of RHA and the ternary blend of CC and RHA specimens is the continuous transition of Ca²⁺ from the PLC matrix to RHA, which enhance the pozzolanic reactivity of the RHA blended SCC and improve its compressive strength [76].

Figure 20. Compressive strength development of SCC specimens.

Figure 20. Compressive strength development of SCC specimens.

4.6. Rapid chloride resistance of SCC

The depth of chloride penetration and migration coefficient of all SCC specimens are shown in Figure 21. The depth of chloride penetration of SCC-1 is 26 mm and increases to 30 mm for SCC-1-20CC. SCC-1-20RHA had the lowest chloride penetration depth of 13 mm, while that of SCC-1-10CC+10RHA was 19 mm. There is no significant difference between the chloride migration coefficient of SCC-1 and SCC-1-20CC, 16 × 10^-12. SCC-1-20RHA had a chloride migration coefficient of 4.5 × 10^-12 and increased to 8.2 × 10^-12 for SCC-1-10CC+10RHA.

SCC-1-20CC achieved similar performance to SCC-1 in terms of chloride migration resistance, although the chloride penetration depth of SCC-1-20CC is greater than that of SCC-1, but the determination of chloride migration resistance according to [47] considers other factors, such as the duration of the test and the voltage used, which give an indication for the density of a concrete microstructure. Both SCC-1 and SCC-1-20CC can be classified as having “Normal” SCC quality - 8 – 16 × 10² m²/s - according to non-steady state chloride migration resistance concrete classification [77,78]. SCC-1-20RHA and SCC-1-10CC+10RHA achieved a “Good” SCC quality due the pozzolanic reactivity of RHA that consumed CH from PLC hydration and produced more C-S-H, which densified the concrete microstructure and improved its chloride resistance.

5. Summary and conclusions

The study investigated the potential use of up to 40 vol-% CC and RHA as a partial replacement for PLC in SCP. Partial replacement of PLC with CC, as used in this study, is possible up to 40 vol% and can be achieved with the same V_w/V_p used for the PLC system, with an increase in SP dosages. The use of RHA as a partial replacement for PLC, on the other hand, requires urgent adjustment of the V_w/V_p even at a lower replacement level of 5 vol-% to achieve similar deformability to the PLC systems; SP adjustment alone cannot provide the required degree of deformability. Therefore, for the application in SCC, the partial replacement of PLC by RHA should be kept at 20 vol-%.

By adjusting the SP dosages, self-compactability can be achieved with PLC partial replacement with 20 vol-%CC, 20 vol-% RHA and 10 vol-% CC + 10 vol-% RHA, using a V_w/V_p = 1.275.

The deformability and short-term segregation resistance of the binary and ternary mix design with 20 vol-% CC, 20 vol-% RHA and 10 vol-% CC + 10 vol-% RHA are within acceptable limits and therefore, the binary and ternary blends of CC and RHA could use in practice up to 20 vol-% as PLC partial replacement.

At an increased SP dosage, PLC partial replacement with 20 vol-% CC has less impact than the binary and ternary blend of 20 vol-% RHA and 10 vol-% CC + 10 vol-% RHA on time dependent workability retention of SCC up to 60 min and therefore, SCC-1-20CC can be used to produce both precast and ready-mix SCC. However, the use of 20 vol-% RHA and the ternary blend 10CC+10RHA developed high flow resistance and showed rapid loss of workability after 30 min of mixing. Therefore, their workability retention needs to be improved for applications beyond 30 minutes. SCC with high content of RHA, 20 vol-% and above, is recommended for the production of precast SCC elements only, due to short workability retention window required by precast SCC compared to ready-mix SCC. Although additional treatment may be required to improve early age strength development of RHA SCC.

SCC produced with RHA as PLC partial replacement showed higher flow resistance and viscosity and increases both the static and dynamic yield stress of SCC. This effect is reduced to some extent by ternary blending CC and RHA. Therefore, the proportion of RHA shall always be kept low, perhaps at 5 vol-%, in the binary and ternary blended SCC mixture, when time dependent workability retention beyond 30 min is required, for example in the ready-mix concrete.

Both CC and RHA consumed CH due to their pozzolanic reactivity. Partial replacement of 20 vol-% PLC with CC had no significant effect on the 28 days compressive strength and chloride migration resistance of SCC. While the SCC produced with RHA and the blend of CC and RHA increased the 28-days compressive strength of SCC by 5 %. The chloride migration resistance of 20 vol-% RHA is 3 times that of SCC produced with only PLC, while that of the ternary blend 10 vol-% CC + 10 vol-% RHA is 2 times that of SCC produced with only PLC. RHA is capable of improving the chloride migration resistance of SCC and should be use to improve the microstructural densification of SCC produced with only PLC.