Advances in Civil Engineering
Volume 2020 (2020), Article ID 8873308, 8 pages
https://doi.org/10.1155/2020/8873308

Research Article

Experimental Research Based on the Optical Fiber Sensing Technology for a Jacked PHC Pipe Pile Penetration Process

Songkui Sang, Yonghong Wang, Jiaxiao Ma, and Mingyi Zhang

School of Civil Engineering, Qingdao University of Technology, Qingdao, China

Correspondence should be addressed to Yonghong Wang; wangyonghong@edu.qut.cn

Received 23 April 2020; Revised 29 May 2020; Accepted 15 June 2020; Published 8 July 2020

Academic Editor: Yixian Wang

Copyright © 2020 Songkui Sang et al. 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.

Abstract.

The aim of this work is to explore the influence of the end resistance and shaft resistance regarding the mechanism for jacked pile penetration and the load-transfer rule during the penetration process. A full-scale field test was conducted in an actual project located in Dongying, Shandong Province, China. In this test, the axial strain experienced by two closed Prestressed High-strength Concrete (PHC) pipe piles during jacking into layered soil was monitored successfully using Fiber Bragg Grating (FBG) sensors mounted on the pile shaft. The experimental results show that FBG sensors have a good stability, strong antijamming performance, and can effectively monitor the pile stress. The variation law of the jacking force reflects the distribution of the soil layer, and the hardness of the soil layer at the pile end limits the pile force. When the pile end enters the silt layer from the clay layer, the jacking force and shaft resistance increase by 2.5 and 1.7, respectively. The shaft resistance accounted for 44.99% of the jacking force. The end resistance is affected by the mechanical properties of soil, and the end resistance of the silt layer is approximately twice that of the clay layer. The end resistance of the silt layer accounted for 59.84% of the jacking force. When the pile end enters the soft soil layer from the hard soil layer, the impact of the pile driving speed and the tangential force on the surface of the pile body must both be considered. During the pile penetration process, as the penetration depth increases, the radial stress on the pile side at a given depth is gradually released, while the shaft resistance at the pile side degrades significantly.

1. Introduction

A Prestressed High-strength Concrete (PHC) pipe pile is a hollow cylindrical precast concrete member produced by pretension prestressing, centrifugal techniques, and high temperature curing [1–4]. PHC pipe piles are widely used in foundation works in civil, municipal, and other projects in China due to the advantages of a high bearing capacity, high construction efficiency, and reliable quality [5–8]. The hydraulic jacking method is a common technique for pile penetration that has several advantages such as being vibration-free and noise-free during construction [9–12]. This method is generally used to press a PHC pipe pile into the site soil.

In the recent years, fiber optic sensing technologies have developed rapidly, and various sensors based on the fiber optic sensing technology are widely used in engineering monitoring [13–19]. Compared with traditional sensors such as strain gauges, fiber optic sensing technology has the advantages of a high test accuracy, strong anti-interference ability, and wide monitoring rang [20–24]. Scholars around the world have conducted thorough research on the strain distribution and penetration characteristics of piles using fiber optic sensors. Klar et al. [25] adhered optical fibers to steel reinforcing bars of a pile to monitor their performance based on the Brillouin optical time domain reflectometer (BOTDR) technology. Lu et al. [26] measured the strain of precast concrete piles using optical fibers based on the BOTDR technology. Ding et al. [27] monitored the strain of an H-pile in SWM based on the Brillouin optical time domain analysis (BOTDA) technology. Guo et al. [28] adopted Brillouin optical frequency domain analysis (BOFDA) technology with a steel stress meter to monitor the strain, stress, and axial force of a bridge pile foundation.

To further improve the accuracy and resolution of the tests, Fiber Bragg Grating (FBG) sensors have been used to monitor the stress and strain of pile foundations. Lee et al. [29] measured the strain of a PHC pipe pile during static load testing based on the FBG strain sensors and strain gauges. Weng et al. [30] installed FBG strain sensors on the surface of the pile using an epoxy resin to monitor the strain state of the model pile during centrifugal testing. Baldwin et al. [31] installed FBG sensors in the shallow grooves of a pile and protected the sensors using an epoxy resin. Schilder et al. [32] measured the strain in concrete piles under static and dynamic loads based on FBG strain sensors to evaluate the bearing capacity. Liu et al. [33] monitored the end and shaft resistances of an open-ended PHC pipe pile using FBG strain sensors. Doherty et al. [34] adopted FBG sensors to measure the strain of precast piles and steel pipe piles and found that these sensors can well meet the testing requirements for different pile foundations. The central wavelength of FBG sensors is influenced by the temperature and strain [35–37]. However, the influence of temperature changes on the accuracy of the FBG strain sensor is often ignored in the existing studies. To improve the monitoring accuracy of FBG strain sensors in pile tests, the temperature should be compensated for, especially in cold regions.

To investigate the capacity properties of closed PHC pipe piles during penetration into a layered stratum, a full-scale test was conduct based on an actual project located in Shandong province, China. The low-temperature sensitive, FBG strain sensors, and FBG temperature sensors were installed in the shallow grooves along opposite sides of the PHC pipe piles. Thus, the strain of the PHC pipe piles can be measured to avoid the effects of temperature under hydraulic driving. Thus, the axial force, end resistance, shaft resistance, and unit shaft resistance of the PHC pipe pile under hydraulic driving can be calculated. The research results can provide reference and guidance for jacked pile engineering in a cold region.

2. Site Conditions and Test Program

2.1. Site Conditions

The test site is situated in Dongying City, Shandong Province, China, in the quaternary alluvial plain landform of the Yellow River Delta. The surface layer is backfill soil with a thickness of 0.9–5.3 m, and the buried depth of the groundwater level is 0.30–3.00 m. The soil parameters of the test site are as shown in Table 1.

Table 1: Soil parameter.

Soil type
Soil description
Thickness (m)
Water content, ω (%)
Unit weight, γ (kN/m³)
Void ratio, e₀
Cohesion, c (kPa)
Internal friction angle, ϕ (o)
Compression modulus, Es (MPa)

Fill
Plastic clay
0.9–5.3
30.6
18.5
0.867
13.8
6.8
4.1

Silty soil A1
Loose dense silty soil
0.3–2.5
28.8
18.6
0.803
8.7
20.1
8.1

Silty clay B1
Soft plastic clay
0.3–1.9
30.9
18.3
0.876
17.6
7.4
4.8

Silty soil A2
Medium dense silty soil
0.3–4.0
28.3
18.7
0.794
8.7
21
8.7

Silty clay B2
Soft plastic to flow plastic clay
2.6–4.6
31.7
18.3
0.895
17.5
6.8
4.6

Silty soil A3
Medium dense silty soil
0.8–3.8
28.3
18.7
0.793
10.3
20.6
10.2

Note. c and ϕ were determined using the quick shear tests, and Es was determined using the one-dimensional compressibility test; the thickness was obtained by the auger boring test.

2.2. Installation of PHC Pipe Piles with FBG Sensors for Field Monitoring

In the tests, the PHC-A400 (95) prestressed high-strength concrete pipe pile was used for testing. The pile length was 12 m, Young’ modulus was 36 GPa, axial compressive strength was 35.9 MPa, and the tested piles are denoted as P1 and P2. Before installing the sensors, a mark was placed on the pile body, and a slotting machine was used to make a shallow groove at a depth of 2 cm and a width of 4 cm. After slotting, the sensor position was leveled to avoid eccentrically compressing the sensors during pile pressing. The support of the sensor was fixed in the shallow groove using epoxy resin, and the FBG sensor was installed after the epoxy resin hardened. After the sensors were installed, the shallow groove was filled with epoxy resin and made flush with the surface of the pile body. The cable of the FBG sensor was led out from the drilled hole on the top of the pile. The procedures for the installation are shown in Figure 1.

(a)

(b)

(c)

(d)

Figure 1: FBG sensor installation process: (a) marking the sensor locations; (b) slotting with a machining tool, (c) installing the sensor, and (d) sealing with epoxy resin.

In the test, six FBG strain sensors and FBG temperature sensors were installed in one side along the pile, and another seven FBG sensors were at the opposite side. The installation positions of the FBG sensors are as shown in Figure 2. The performance parameters of FBG sensors are as shown in Table 2. The distance of center of the sensor closest to the pile end was 20 cm from the pile end to avoid the influence of the pile end plate on the measurement.

Figure 2: Installation position of the FBG sensors.

Table 2: The performance parameters of FBG sensors.

Sensor sleeve
Working temperature (°C)
Strain range (ε)
Gage (mm)
Strain resolution
Centre wavelength

Armor sheath
−30∼120
±1500
60
1
1510∼1570

The test used a 680-ton hydraulic pile driver with a maximum stroke of 1.8 m. It was difficult to control the penetration rate at a fixed value as the penetration depth increased during the process. The pile penetration speed was approximately 1.8–3 m/min. At the initial stage of pile penetration, the lower penetration resistance caused the pile penetration speed to be slightly larger. As the penetration depth increased, the resistance to penetration gradually increased and reduced the pressing speed. Bond et al. [38] defined a penetration rate of more than 0.4–0.6 m/min as a fast penetration and a penetration rate of 0.005–0.10 m/min as a slow penetration. In this test, the pile jacking process is considered as fast penetration. In the penetration process, the pile length was used as the final pressure control standard. The test data were collected using the FS 2200RM-Rack-Mountable Bragg Meter demodulator produced by Portugal, which directly collected the wavelength difference from the center wavelength of the fiber grating.

3. Test Results and Discussion

3.1. Variation of Jacking Force with Penetration Depth

As shown in Figure 3, the jacking forces increased with the penetration depth. The jacking forces of P1 and P2 show similar characteristics with the penetration depths from 0–5.0 m. The jacking forces of P1 and P2 increased by factors of approximately 2.8 and 2.2 with the penetration depth from 5.0–7.8 m and 7.9 m, respectively, because the resistance of silty soil was greater and the jacking force must be increased to further press the pile into the soil. When the pile end penetrated the silty clay layer, the jacking force decreased: P1 decreased from 1160 to 778 kN, and P2 decreased from 855 to 564 kN. The penetration resistance is mainly determined by the average strength of the soil layer within 2.5D below the pile end, which is the main reason for differences in the jacking forces between P1 and P2. This indicates that the jacking force is affected primarily by the type of soil layer at the end of the pile.

Figure 3: Jacking force versus penetration depth.

3.2. Variation of Axial Force with Penetration Depth at Six Penetration Depths

Through the wavelength difference of sensors measured, the axial strain ε of the pile can be calculated by

where ΔλB is the wavelength difference; λB is the center wavelength of the reflected light; Sε is the strain sensitivity coefficients with S = 1−Pe = 0.784/με; Pe is the valid elastic-optic constant; and ε is the axial strain of the pile.

In the test, FBG strain sensors were installed on both sides of the pile, and the axial strain of the pile at level i can be calculated by

where εNi is the average axial strain of the pile at level i (i = 1, …, 6) and εFBGi and εFBGi’ are the axial strains measured by two FBG strain sensors installed at the same depth.

The axial force Fi (i = 1, …, 6) of the pile at section i can be calculated by

where Ap is the cross-sectional area of the pile and Ep is Young’s modulus.

As shown in Figure 4, the axial forces of P1 and P2 at 1.0, 2.0, 3.0, 6.5, 8.0, and 16.0 m penetration depths are calculated using equation (3). The axial forces of P1 and P2 at a given soil depth increase with the penetration depth from 1.0–2.0 m until 12.0 m. The trend of the axial force in Figure 4(a) for P1 is similar to that of Figure 4(b) for P2 except for a few differences in the values. The axial forces along the piles decrease with the distance from the pile head at a given penetration depth. This indicates that the axial forces are related to both the penetration depth and the shaft resistance.

(a)

(b)

Figure 4: Axial force profiles along the piles at different penetration depths: axial forces of (a) P1 and (b) P2.

3.3. Variation of End and Shaft Resistances with Penetration Depth

As shown in Figure 5, the end resistances of P1 and P2 increased with the penetration depth. The end resistances were obtained from the value of the sensor near the bottom of pile. The trends in Figure 5 for P1 are similar to those for P2 with some differences. When the pile end penetrated the silty soil layer, the end resistance increased: P1 increased from 365 to 735 kN and P2 increased from 234 to 490 kN. In order to reduce the influence between P1 and P2 piles, the pile distance is set to 2.0 m, which is the reason for the large difference between P1 and P2 piles. This can be explained as the end resistances being affected by the soil layer at the different pile positions.

Figure 5: End resistance versus penetration depth.

As shown in Figure 6, when the penetration depth was 0–3.0 m, the shaft resistances for P1 and P2 increased slowly. This is because pile sloshing and shallow soil uplift cause the pile-soil interface contact to be loose with a small radial effective stress. When the penetration depth was around 4 m (when the pile end entered the silty clay layer from the silt layer), the shaft resistance initially decreased and then increased. This is because the end of the pile entered the clay layer, which suddenly decreased the end resistance of the pile. The pressing speed of the pile increased sharply, and there was a thick mud film between the pile and the soil, which reduced the shaft resistance of the pile. The decreased end resistance of the pile caused an increased tangential force of the pile body and increased the adhesion force between the pile and the soil.

Figure 6: Shaft resistance versus penetration depth.

3.4. Variation of Unit Shaft Resistance with Penetration Depth

The unit shaft resistance of the pile can be calculated as

where Fi is the axial force at level i, Fi-1 is the axial forces at level i−1, hi−hi−1 is the distance between levels i and i−1, and D₀ is the external diameter of the pile.

As shown in Figures 7(a) and 7(b), the unit shaft resistances of P1 and P2 at penetration depths of 3.0, 6.5, 8.0, and 12.0 m can be calculated from equation (4). The unit shaft resistances of the piles at a given penetration depth does not increase gradually with the distance from the pile head. The trends of the unit shaft resistances for P1 and P2 in Figures 7(a) and 7(b) are distinct, but with some similarities. This indicates that the unit shaft resistances are related to the distribution and parameters of the soil layers. The unit shaft resistance at a given soil depth decreased with the penetration depth from 3.0–6.5 m until 12.0 m. This can be explained as the side soil of the pile at a given soil depth was continuously sheared and squeezed by the pile, which disturbed the soil and decreased the shear strength.

(a)

(b)

Figure 7: Unit shaft resistance along piles at different penetration depths: unit shaft resistances of (a) P1 and (b) P2.

4. Summary and Findings

This paper monitored the strain and temperature state of PHC pipe piles during jacking using low-temperature sensitive, FBG, strain sensors, and FBG temperature sensors. The following conclusions are drawn.

(1)The low-temperature sensitive, FBG strain sensors, and FBG temperature sensors were installed on the surface of PHC pipe pile using the slot-embedding method. The installation method of the sensors improved their survival rate. The low-temperature sensitive, FBG, and strain sensors used in this study can better satisfy the monitoring requirements of PHC pipe pile penetration characteristics during jacking than traditional approaches.(2)The distribution of the soil layers affects the jacking force and end resistance, and the change laws of the jacking force and end resistance with depth reflect the soil layer distributions. When the pile end penetrated the silty clay layer, the jacking force and end resistance increased by factors of 2.5 and 2, respectively.(3)At a given depth, as the penetration depth of the PHC pipe pile increased, the pile and soil continuously sheared each other and the radial stress on the side of the pile gradually released. This resulted in a decreased unit shaft resistance. The shaft resistance gradually deteriorated, which caused the unit shaft resistance of the piles to gradually decrease and show a significant degradation.

Data Availability

The Microsoft Excel Worksheet data used to support the findings of this study are available from the corresponding author (wangyonghong@edu.qut.cn) upon request.

Conflicts of Interest

The authors declare that they have no conflicts of interest.

Acknowledgments

This research was supported financially by the National Natural Science Foundation of China (51708316, 51778312, and 51809146) and the Shandong Province Emphasis Research Program, China (2017GSF16107, 2018GSF117010, and 2018GSF117008).

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