Use of Nanosilica for Increasing Dune Erosion Resistance during a Sea Storm

: Dune recovery interventions that integrate natural, sustainable, and soft solutions have become increasingly popular in coastal communities. In the present study, the reliability of an innovative non-toxic colloidal silica-based solution for coastal sand dunes has been veriﬁed for the ﬁrst time by means of laboratory experiments. An extensive experimental campaign aimed at studying the effectiveness of the use of nanosilica has been conducted in the 2D wave ﬂume of the EUMER laboratory at the University of Salento (Italy). The study was ﬁrst based on a horizontal seabed and then a cross-shore beach-dune proﬁle was drawn similar to those generally observed in nature. Detailed measurements of wave characteristics and observed bed and cross-shore beach-dune proﬁles were analyzed for a wide range of wave conditions. In both cases, two sets of experiments were carried out. After the ﬁrst set of experiments performed resembling the native conditions of the models composed with natural sand, the effects of the injection of the mineral colloidal silica-based grout were investigated. The observations show that mineral colloidal silica increases the mechanical strength of non-cohesive sediments reducing the volume of dune erosion, thus improving the resistance and longevity of the beach-dune system. proﬁles of a beach-dune system observed for seven different wave conditions in the case of natural sand and consolidated sand were compared. It was observed that, with the injection of the consolidating nanosilica-based grout, the cross-shore dune proﬁle under ﬁve wave attacks remained practically unchanged; under the other two wave attacks, a delay in the erosion process was observed. The results demonstrate signiﬁcant advantages in the use of nanosilica to improve erosion resistance of the dune.


Introduction
The continuously growing human population along the coasts of the world will aggravate the impact of human activities on the coastal environments [1]. Therefore, defensive and restoration activities of coastal areas will become increasingly important [2]. Sandy dunes constitute the natural barrier protecting coastal environments against flooding due to storm surge and wave impacts. The process of defense and restoration consists in preventing degradation and assisting the recovery of an ecosystem that has been damaged or destroyed with respect to its health, integrity, and sustainability [3][4][5]. In the last decades, several soft and hard engineering solutions dealing with coastal dune erosion prevention have been proposed [6,7]. Despite the results in terms of erosion reduction obtained by the installation of engineering structures, a significant alteration of geomorphological processes is rather unavoidable. To improve traditional construction techniques that used rock, concrete, and steel, new alternative techniques are proposed, using geosynthetic materials for revetments, scour protection, and reclamation [8]. In this regard, planting vegetation and/or constructing plant fences along the backshore was found to be a more natural solution. Installation of planted vegetation limits the mobility of the sand caused by aeolian forces or wave action [9,10]. Nevertheless, a recurrent issue that is addressed in restoration using plants is counteracting the negative impact of depressed biodiversity and even loss of endemic species [11,12]. Moreover, great care must be taken when dealing with changes in geomorphological processes. The collective movement of solid particles, known as sediment transport, is a complex problem related to flow conditions, the nature of the sediment, and the cohesive forces between particles. Historical overviews of the influence of wave conditions, sediment size, sediment gradation, etc., have been extensively studied, for example, by Jonsson [13], Madsen and Grant [14], Sleath [15], Nielsen [16], Fredsøe and Deigaard [17], Van Rijn [18], Soulsby [19], and cross-shore wave mechanics and sediment transport on beaches has been investigated by Nairn and Southgate [20], Kobayashi and Johnson [21], Dean and Dalrymple [22], Tomasicchio et al. [23,24], D'Alessandro and Tomasicchio [25], D'Alessandro et al. [26], Sancho et al. [27], and Brunone and Tomasicchio [28]. These works show the wave-induced bottom shear stress as an essential parameter for calculation of beach erosion and accretion rate and wave height attenuation.
In the present study, the use of nanosilica for coastal sand dune strengthening has been evaluated in the 2D wave flume of EUMER at Unisalento, Lecce (www.eumer.eu, accessed on 10 September 2019). The method concerns the injection of a colloidal silica-based solution into the sand in order to obtain a consolidated layer and reduce the erosion process due to wave action. Testing the performance of the use of nanosilica included two stages. In the first stage, wave-driven sand transport was measured on a mobile sand bed for a wide range of flow conditions. The bed with natural well-sorted fine sand was compared with the bed with the silica-based consolidating material, which changed the cohesive properties of the sand. Observing the behavior of both the natural and consolidated sand has clarified the relationship between the sand properties and hydrodynamic loadings (e.g., bed shear stress). Thereafter, physical model tests on the morphological development of the beach-dune system under irregular waves were conducted with the aim of observing and comparing the behavior of natural and consolidated sand. The conducted experiments, including setup, data analysis, and comparison of the data are presented in the following sections.

Experimental Facility
In the framework of the INNODUNE project, physical model tests were conducted in a 2D wave flume at the EUMER lab, Campus Ecotekne, Lecce ( Figure 1). The flume is 45 m long, 1.5 m wide, and 2 m deep. The wave generation is performed by a single paddle equipped with an active wave absorption system allowing tests to be run without the effect of spurious model-induced reflections. Froude's law was selected as the proper criterion to down-scale the hydrodynamic parameters; however, on fine-grained sand beaches, the geometric scaling leading to a clay-size sediment were avoided to prevent the inception of cohesive effects [29]. Therefore, the grain size of the sediment in the flume is not scaled by the geometric scale, resulting in the same sand in the model [30]. The sediment is well-sorted fine sand with a median diameter d 50 of 0.245 mm. The measured density of sediment grains, ρ s , and porosity, ε, of the sand are 2.6 g/cm 3 and 0.4, respectively. The experimental program involved measurements of time-varying water level and bed profile. A wave gauge system from HR Wallingford acquired the water level with an accuracy of the order of 0.1 mm [31], enabling both statistical and spectral analysis of the waves through the HR DAQ data acquisition and analysis software program.
The cross-shore profile is observed with the laser profiler described by HR Wallingford. The system consists of a vertical position controlled device driven by a small electric motor with a mechanical transmission actuating a rod. At the lower end of the rod, a low-powered laser distance sensor mounted inside a waterproof housing is provided. The position of the probe is measured by encoders on the moto shafts, leading to the observation of the bed height, even rather inclined and irregular profile, with an accuracy of the order of 0.1 mm [32]. The bed profile observation is performed by the horizontal motion of the vertical servo controlled device placed in a carriage. The cross-shore profile is observed with the laser profiler described by HR Wallingford. The system consists of a vertical position controlled device driven by a small electric motor with a mechanical transmission actuating a rod. At the lower end of the rod, a low-powered laser distance sensor mounted inside a waterproof housing is provided. The position of the probe is measured by encoders on the moto shafts, leading to the observation of the bed height, even rather inclined and irregular profile, with an accuracy of the order of 0.1 mm [32]. The bed profile observation is performed by the horizontal motion of the vertical servo controlled device placed in a carriage.

Nanosilica-Based Grout
The additive to consolidate the sand consists of a non-toxic aqueous suspension with dispersed nanometric particles of colloidal silica ( Figure 2). These particles are made of quartz (SiO2) with a tetrahedral distribution of the atoms which makes the mixture completely mineral, highly reactive, and more stable than other quartz-based crystalline compounds. Before injecting nanosilica into the sand, an accelerator, i.e., a solution of sodium chloride (10% NaCl in water), is added to the suspension. The solution acts as an activator, triggering a gelification process that induces the suspension to become a gel. Depending on the dosage, the accelerator adjusts the product workability time [33]. Nanosilica, before gelation, has a very low viscosity (very close to water: about 10 mPa·s compared to 1 mPa·s), which means a very high permeation and penetration capacity.
After mixing the components, the dispersion of the nanosilica-based grout was carried out by a pressure pulverizer at 20 °C, penetrating into the surface layer of the sand.

Nanosilica-Based Grout
The additive to consolidate the sand consists of a non-toxic aqueous suspension with dispersed nanometric particles of colloidal silica ( Figure 2). These particles are made of quartz (SiO 2 ) with a tetrahedral distribution of the atoms which makes the mixture completely mineral, highly reactive, and more stable than other quartz-based crystalline compounds. Before injecting nanosilica into the sand, an accelerator, i.e., a solution of sodium chloride (10% NaCl in water), is added to the suspension. The cross-shore profile is observed with the laser profiler described by HR Wallingford. The system consists of a vertical position controlled device driven by a small electric motor with a mechanical transmission actuating a rod. At the lower end of the rod, a low-powered laser distance sensor mounted inside a waterproof housing is provided. The position of the probe is measured by encoders on the moto shafts, leading to the observation of the bed height, even rather inclined and irregular profile, with an accuracy of the order of 0.1 mm [32]. The bed profile observation is performed by the horizontal motion of the vertical servo controlled device placed in a carriage.

Nanosilica-Based Grout
The additive to consolidate the sand consists of a non-toxic aqueous suspension with dispersed nanometric particles of colloidal silica ( Figure 2). These particles are made of quartz (SiO2) with a tetrahedral distribution of the atoms which makes the mixture completely mineral, highly reactive, and more stable than other quartz-based crystalline compounds. Before injecting nanosilica into the sand, an accelerator, i.e., a solution of sodium chloride (10% NaCl in water), is added to the suspension. The solution acts as an activator, triggering a gelification process that induces the suspension to become a gel. Depending on the dosage, the accelerator adjusts the product workability time [33]. Nanosilica, before gelation, has a very low viscosity (very close to water: about 10 mPa·s compared to 1 mPa·s), which means a very high permeation and penetration capacity.
After mixing the components, the dispersion of the nanosilica-based grout was carried out by a pressure pulverizer at 20 °C, penetrating into the surface layer of the sand. The solution acts as an activator, triggering a gelification process that induces the suspension to become a gel. Depending on the dosage, the accelerator adjusts the product workability time [33]. Nanosilica, before gelation, has a very low viscosity (very close to water: about 10 mPa·s compared to 1 mPa·s), which means a very high permeation and penetration capacity.
After mixing the components, the dispersion of the nanosilica-based grout was carried out by a pressure pulverizer at 20 • C, penetrating into the surface layer of the sand. After spraying the grout and completion of the gelling time, a homogeneous consolidation of the sand was observed. The result consisted of a pore-filling process and an increase in cohesion of the sand; nevertheless, the nanosilica-based material did not interfere with germination or seedling growth because permeability was ensured. On a control volume, different amounts of nanosilica were tested, defined by a percentage of the grout relative to the voids in the sand. In particular, tested amounts were 5%, 2%, and 1% which resulted in a consolidated sand layer of different depth, h c , and porosity ε (Table 1). In Figure 3, samples of consolidated layers are shown. After spraying the grout and completion of the gelling time, a homogeneous consolidation of the sand was observed. The result consisted of a pore-filling process and an increase in cohesion of the sand; nevertheless, the nanosilica-based material did not interfere with germination or seedling growth because permeability was ensured. On a control volume, different amounts of nanosilica were tested, defined by a percentage of the grout relative to the voids in the sand. In particular, tested amounts were 5%, 2%, and 1% which resulted in a consolidated sand layer of different depth, hc, and porosity ε (Table 1). In Figure 3, samples of consolidated layers are shown.

Horizontal Bed Experiments
The first part of the experimental campaign was carried out on a horizontal seabed. The experiment was conducted because the wave boundary layer on a horizontal bed is well understood. The bottom shear stress on natural and consolidated sands can be estimated using existing wave boundary layer models. In the wave flume, two concrete blocks with a triangular transversal geometry and 1:3 slope were positioned at a distance of 2 m from each other. The blocks were 0.3 m high, 0.9 m long, and as wide as the width of the flume. The 2-m gap between the blocks was filled with sand. A picture of the first physical model is shown in Figure 4.

Horizontal Bed Experiments
The first part of the experimental campaign was carried out on a horizontal seabed. The experiment was conducted because the wave boundary layer on a horizontal bed is well understood. The bottom shear stress on natural and consolidated sands can be estimated using existing wave boundary layer models. In the wave flume, two concrete blocks with a triangular transversal geometry and 1:3 slope were positioned at a distance of 2 m from each other. The blocks were 0.3 m high, 0.9 m long, and as wide as the width of the flume. The 2-m gap between the blocks was filled with sand. A picture of the first physical model is shown in Figure 4. After spraying the grout and completion of the gelling time, a homogeneous consolidation of the sand was observed. The result consisted of a pore-filling process and an increase in cohesion of the sand; nevertheless, the nanosilica-based material did not interfere with germination or seedling growth because permeability was ensured. On a control volume, different amounts of nanosilica were tested, defined by a percentage of the grout relative to the voids in the sand. In particular, tested amounts were 5%, 2%, and 1% which resulted in a consolidated sand layer of different depth, hc, and porosity ε (Table 1). In Figure 3, samples of consolidated layers are shown.

Horizontal Bed Experiments
The first part of the experimental campaign was carried out on a horizontal seabed. The experiment was conducted because the wave boundary layer on a horizontal bed is well understood. The bottom shear stress on natural and consolidated sands can be estimated using existing wave boundary layer models. In the wave flume, two concrete blocks with a triangular transversal geometry and 1:3 slope were positioned at a distance of 2 m from each other. The blocks were 0.3 m high, 0.9 m long, and as wide as the width of the flume. The 2-m gap between the blocks was filled with sand. A picture of the first physical model is shown in Figure 4.  One wave gauge (WG1) was located as close as possible to the wave generator and three wave gauges (WG2-WG4) were used to evaluate the wave conditions over the horizontal seabed and to separate incident and reflected waves in the wave flume. The bed profile was observed with the laser profiler for an extension of 1.5 m on the seabed to avoid the edge effects due to the slopes. A side view of the full experimental setup is shown in Figure 5.
ar. Sci. Eng. 2021, 9, x FOR PEER REVIEW 5 of 18 One wave gauge (WG1) was located as close as possible to the wave generator and three wave gauges (WG2-WG4) were used to evaluate the wave conditions over the horizontal seabed and to separate incident and reflected waves in the wave flume. The bed profile was observed with the laser profiler for an extension of 1.5 m on the seabed to avoid the edge effects due to the slopes. A side view of the full experimental setup is shown in Figure 5. Non-breaking wave conditions were adopted. Regular and irregular wave tests were conducted on the horizontal seabed. The incident and reflected wave parameters were obtained using the theory of Mansard and Funke [34]. The reflection coefficient, kr, defined as the ratio between the reflected and incident wave height was less than 0.25. Table 2 lists the incident wave characteristics in sequence. In particular, tests marked with HN (Horizontal Natural) refer to a movable bottom of natural sand without adding colloidal nanosilica. Tests marked with HC (Horizontal Consolidated) refer to a condition of sand with a percentage of nanosilica calculated so as to achieve a consolidated sand layer of 5 cm. The regular wave conditions are defined by wave height, H, and wave period, T. The irregular wave conditions are based on a Jonswap spectrum with peak enhancement factor, γ, equal to 3.3, and defined by energy-based significant wave height, Hm0, and peak period, Tp. Three water depths above the bed, h, were chosen, starting from 0.4 m increased by 0.1 m up to 0.6 m. The water depth in front of the wave generator was (h + 0.3) m. Two tests of regular waves and two tests of irregular waves were carried out for each h. The duration of wave attacks was defined considering the time required for bed form to develop evenly along the seabed [35]. In particular, for regular waves, a number of waves were specified to be generated; under irregular waves, the bed forms may grow slowly, especially under low velocities that are not much above threshold. Some exploratory experiments were conducted to determine the necessary durations. In both cases, the total duration also includes the time the wave takes to reach the model and return to the wave generator which, for convenience, has been associated with the duration of 30 waves. This calculated time was excluded during wave data analysis [35]. Non-breaking wave conditions were adopted. Regular and irregular wave tests were conducted on the horizontal seabed. The incident and reflected wave parameters were obtained using the theory of Mansard and Funke [34]. The reflection coefficient, k r , defined as the ratio between the reflected and incident wave height was less than 0.25. Table 2 lists the incident wave characteristics in sequence. In particular, tests marked with HN (Horizontal Natural) refer to a movable bottom of natural sand without adding colloidal nanosilica. Tests marked with HC (Horizontal Consolidated) refer to a condition of sand with a percentage of nanosilica calculated so as to achieve a consolidated sand layer of 5 cm. The regular wave conditions are defined by wave height, H, and wave period, T. The irregular wave conditions are based on a Jonswap spectrum with peak enhancement factor, γ, equal to 3.3, and defined by energy-based significant wave height, H m0 , and peak period, T p . Three water depths above the bed, h, were chosen, starting from 0.4 m increased by 0.1 m up to 0.6 m. The water depth in front of the wave generator was (h + 0.3) m. Two tests of regular waves and two tests of irregular waves were carried out for each h. The duration of wave attacks was defined considering the time required for bed form to develop evenly along the seabed [35]. In particular, for regular waves, a number of waves were specified to be generated; under irregular waves, the bed forms may grow slowly, especially under low velocities that are not much above threshold. Some exploratory experiments were conducted to determine the necessary durations. In both cases, the total duration also includes the time the wave takes to reach the model and return to the wave generator which, for convenience, has been associated with the duration of 30 waves. This calculated time was excluded during wave data analysis [35].
Wave parameters are subject to changes due to wave transformation and wave height may decrease, due to wave energy loss. The intensity of wave energy dissipation depends on the incident wave height, water depth, and bottom characteristics. Using the wave conditions acquired in HC and HN tests, the amplitude of the wave orbital velocity, U w , and one half of the horizontal orbital excursion, A w , just above the bottom boundary layer for regular waves were calculated as [19]: where sinh is the hyperbolic sine, k = 2π L is the wave number, L is the wavelength, and h the water depth over the seabed. For irregular waves, H and T are replaced by H m0 and T p . Bed form conditions responded to increasing wave energy for HN2-12. The measured ripple height and wavelength were estimated about 1 cm and 10 cm, respectively. In the remaining tests (HN1 and HC1-12) the seabed configuration did not change in response to the wave attack, remaining flat.

Movement of Natural and Consolidated Sands
An estimate of the threshold of motion can be given by the Shields parameter, θ 0 , in terms of the ratio of the force exerted by the bed shear stress acting on a grain on the bed, to the submerged weight of the grain counteracting this [19]. The bed shear stress, τ w , represents the most important hydrodynamic property of waves for sediment transport purposes. It is usually obtained from U w and the bottom friction factor, f w . Acting on the bed, τ w is made up of contributions due to the skin friction, τ ws , produced by (and acting on) the sediment grains and the form drag, τ wf , produced by the pressure field associated with the flow over ripples and/or larger features on the bed. If the bed is flat and sediment transport is not intense, the distinction between total and skin friction quantities is not necessary. It is important to be aware that only the skin friction contribution acts directly on the sediment grains, and the skin friction is normally used to calculate the threshold of motion, bedload transport, and reference concentration or pick-up rate for grains in suspension. On the other hand, it is the total bed shear stress that corresponds to the overall resistance of the flow and determines the turbulence intensities which influence the diffusion of suspended sediment higher in the water column. In literature, several expressions of f w were found with a great variability in terms of Reynolds number, Re = A w U w ν , where ν is the kinematic viscosity, and the relative roughness, A w k N , where k N is the Nikuradse equivalent bed roughness. k N can be written as sum of grain-related k Ns and form drag k Nf components. Among the available formulas, the formulation by Soulsby [19] was adopted to calculate f w . This is a choice taken by many authors [36][37][38].
The formulation by Soulsby does not depend on the wave Reynolds number, and a rough turbulent bed is assumed. Therefore, θ 0 , τ w , and f w are defined by: where g is the acceleration due to gravity, ρ is the density of the water, and the density and the median diameter of the sand are ρ s =2.6 g/cm 3 and d 50 =0.245 mm in this study.
In the present work, K N is evaluated in the form K N = 2.5 d 50 proposed by Nielsen (1992) [16].
According to Shields, the sediment movement may be observed when a critical value of bed shear stress is reached with a typical value of θ 0 is of about 0.05 [39]. Figure 6 shows the calculated θ 0 for each test considering only the skin friction shear stress contribution which acts directly on the sediment grains.
does not depend on the wave Reynolds number, and a rough turbulent bed is as Therefore, , , and are defined by: where is the acceleration due to gravity, is the density of the water, and the and the median diameter of the sand are = 2.6 g/cm 3 and = 0.245 mm in thi In the present work, KN is evaluated in the form = 2.5 proposed by Nielse [16].
According to Shields, the sediment movement may be observed when a critic of bed shear stress is reached with a typical value of is of about 0.05 [39]. F shows the calculated for each test considering only the skin friction shear str tribution which acts directly on the sediment grains. for HN and HC test groups as a function of Uw.
In HN tests, the results were consistent with Shield's theory. In tests with than 0.05, mobilization at the bottom was observed. Only in the case of HN1, the = ( − ) = 1 2 Figure 6. θ 0 for HN and HC test groups as a function of U w .
In HN tests, the results were consistent with Shield's theory. In tests with θ 0 greater than 0.05, mobilization at the bottom was observed. Only in the case of HN1, the critical value not reached. On the other hand, in HC tests, although the threshold θ 0 is reached, mobility at the bottom was not observed. In particular, the largest value of θ 0 was observed in the HC4 regular wave test with a duration of 360 s corresponding to a consolidated sand resistance force per unit area of 0.81 N/m 2 . For irregular waves, θ 0 became as large as 0.16 in the HC10 with a duration of 1752 s, reaching a consolidated sand resistance force per unit area of 0.61 N/m 2 .
This experiment indicated the practical utility of nanosilica grout but, since its performance against breaking waves is unknown, new experiments using breaking waves were carried out.

Dune Erosion Experiments
A second part of the experimental campaign consisted of a model beach-dune system located at 23.3 m from the wave generator. The model in the flume had a length of 6.9 m. The beach had a slope of 1/10 by an extension of 5.2 m and a slope of 1/50 by an extension of 0.2 m. The dune length was 1.5 m with a seaward slope of 1/1.5. The dune crest length was 0.5 m, and the dune height above the toe was 0.35 m. These slope gradients are typically observed along the Italian coastline. The still water level (SWL) was chosen in such a way that the part of the beach with a slope of 1/10 was mostly submerged and the part with a slope of 1/50 was fully emerged. Waves were measured using wave gauges WG1-WG7. A side view of the beach-dune system as built with the instrumentation is shown in Figure 7. The origin along the onshore coordinate is taken at WG2. WG1 was located as near as possible to the wave generator to check the accuracy of the wave generation and wave absorption capability of the wave maker. The remaining gauges measured the free surface elevations from the offshore and wave shoaling zones and for reflection analysis following the theory of Mansard and Funke [34]. Given the bathymetry, WG2-WG3-WG4 were placed before the beach and WG5-WG6-WG7 before the dune. In Table 3, the onshore coordinate X (m) and water depth below SWL at each of the seven WGs are listed. a way that the part of the beach with a slope of 1/10 was mostly submerged and the part with a slope of 1/50 was fully emerged. Waves were measured using wave gauges WG1-WG7. A side view of the beach-dune system as built with the instrumentation is shown in Figure 7. The origin along the onshore coordinate is taken at WG2. WG1 was located as near as possible to the wave generator to check the accuracy of the wave generation and wave absorption capability of the wave maker. The remaining gauges measured the free surface elevations from the offshore and wave shoaling zones and for reflection analysis following the theory of Mansard and Funke [34]. Given the bathymetry, WG2-WG3-WG4 were placed before the beach and WG5-WG6-WG7 before the dune. In Table 3, the onshore coordinate X (m) and water depth below SWL at each of the seven WGs are listed.    The cross-shore profile of the beach-dune system is measured with the laser profiler in the zone of noticeable profile changes x = 11.0 m-12.5 m (1.5 m onshore distance). This choice stems from the fact that the nanosilica-based grout was sprayed from the toe up to the crest of the dune to evaluate the increase of the erosion resistance exclusively on the dune face.
Two sets of tests were carried out allowing the observation of the dune erosion process and comparison with the behavior of the system with the nanosilica grout. After the first set of tests, performed resembling the native conditions of the beach-dune system made of natural well-sorted fine sand, the effects of spraying the colloidal silica-based grout over the face of the dune were investigated. Seven dune tests (D) using natural (N) and consolidated (C) sands were carried out. The wave conditions are defined by H m0 and T p at WG 2-4 outside the surf zone and the wave steepness s = 2π H m0 g T 2 p is between 0.01 and 0.07. Starting from time t = 0, the initial profile was exposed to four runs composed of 230, 230, 330, and 330 waves, respectively. The beach profile was measured after each run [35]. Again, 30 waves were excluded during wave data analysis for each run. Table 4 summarizes the incident wave characteristics in the dune erosion experiments.
Reflection coefficients appear relatively large because of the steep dune slope, typically observed along the Italian coastlines and exposed to waves that are not too large. Table 4 shows similar wave characteristics for the corresponding test, DNj and DCj, with j = 1-7. The differences are less than 10% for H m0 , 15% for T p , and 20% for k r .

Erosion of Natural and Consolidated Dunes
In the beach-dune model, incident wave characteristics observed between the offshore and shoaling zones were analyzed to examine the cross-shore wave transformation. In the DN and DC tests, H m0 , T p , and k r at WG 2-4 and WG 5-7 were compared and shown in Figure 8 for all the tests with the four runs. In the beach-dune model, incident wave characteristics observed between the offshore and shoaling zones were analyzed to examine the cross-shore wave transformation. In the DN and DC tests, Hm0, Tp, and kr at WG 2-4 and WG 5-7 were compared and shown in Figure 8 for all the tests with the four runs.
In most of the tests, the wave showed no significant change from WG 2-4 to WG 5-7, except for the DN6-DC6 and DN7-DC7 in which Hm0 decreased due to wave breaking. Comparing the results between the DN and DC tests, kr increased along the flume in the cases of consolidated sand. The above tendencies are associated with the application of nanosilica to the dune, which limits the erosion of the steep dune face. This behavior is most evident in test DC7, where kr increased from about 0.28 at WG 2-4 to about 0.36 at WG 5-7 because of the decrease of Hm0 due to wave breaking. The erosion process of the beach-dune system was observed. Before each new test, the initial conditions of the beach-dune system were restored. It is important to note that it is difficult to exactly reconstruct the same model geometry at the start of each test. Although some geometric parameters were unidentical for all tests (e.g., dune height), the deviation is small enough that they can be considered constant. The process of dune face erosion in the DN tests changed as the test continued. Initially, the slope of the dune face was 1/1.5 (vertical/horizontal). Many waves reach and erode the dune face. The scarped dune front becomes steeper until it is nearly vertical. Then, after a first series of waves In most of the tests, the wave showed no significant change from WG 2-4 to WG 5-7, except for the DN6-DC6 and DN7-DC7 in which H m0 decreased due to wave breaking. Comparing the results between the DN and DC tests, k r increased along the flume in the cases of consolidated sand. The above tendencies are associated with the application of nanosilica to the dune, which limits the erosion of the steep dune face. This behavior is most evident in test DC7, where k r increased from about 0.28 at WG 2-4 to about 0.36 at WG 5-7 because of the decrease of H m0 due to wave breaking.
The erosion process of the beach-dune system was observed. Before each new test, the initial conditions of the beach-dune system were restored. It is important to note that it is difficult to exactly reconstruct the same model geometry at the start of each test. Although some geometric parameters were unidentical for all tests (e.g., dune height), the deviation is small enough that they can be considered constant. The process of dune face erosion in the DN tests changed as the test continued. Initially, the slope of the dune face was 1/1.5 (vertical/horizontal). Many waves reach and erode the dune face. The scarped dune front becomes steeper until it is nearly vertical. Then, after a first series of waves within the first run, a different erosion mechanism starts. The dune face only retreats under waves impacting it. Episodically, the dune face collapses and big lumps of sediment fall or slide down the dune face on the beach in front of the dune. This sand is picked up by swash and inner surf zone processes that move the sediment further seaward extending the new foreshore. At this stage of the erosion process, the number of waves impacting the dune is certainly lower, consequently the erosion rate is reduced. In the DC tests, the injection of the nanosilica protected the surface layer of the dune exposed to run up, so the erosion process did not take place in the first series of waves, as in the DN tests. The dune face remained unchanged for a higher number of waves. A front and side view of the cross-shore profile after four runs of DN4 and DC4 is shown in Figure 9 in order to appreciate the effect of nanosilica on the dune face.  The cross-shore profiles of the beach-dune system were evaluated by the laser profiler attached to a mobile platform with x-axis defined positively onshore from x = 11 m up to x = 12.5 m (see Figure 7). Before the start of each test as well as after every wave run, profiles were recorded along the centerline. The profiler velocity was set in order to have a horizontal resolution of 0.2 mm. Figure 10 presents the comparison of the observed cross-shore profiles of DN4 and DC4.   For the DN4 test, a progressive erosion of the dune face from the first run up to the end of the test was observed. An offshore transport was noticeable from the crest, leading to sand being deposited on the toe of the dune and onto the underlying beach. This is compounded by onshore sand transport increasing sand accumulation at the toe area. Focusing on the DC4 test, it is evident that the cross-shore profile of the dune face did not changed as a result of the injection of the nano-silica based grout. Only the onshore transport was observed, leading to accumulation (of a lower magnitude than DN4) at the toe of the dune and erosion in the inner surf zone.
Erosion progression of the dune was analyzed in order to quantify the effect of the nanosilica-based grout on the dune surface. The eroded area, A e , after each run of the DN and DC tests was normalized by the square of H m0 observed at WG 2-4. Table 5 lists the sequence of the normalized area A * = A e H 2 m0 and the wave steepness s based on H m0 and T p at WG 2-4 for the DN and DC tests. Figure 11 shows A * as a function of s for tests DN1-DN7 for increasing number of waves. Empirical formula for dune erosion can be found for s = 0.012 − 0.068 by fitting an exponential function of the observed data for each number of waves as: where the subscript n indicates that the formula is valid for tests with natural sand, N is the number of waves from 230 to 1120, and a and b are the exponential function coefficients listed in Table 6.
where the subscript n indicates that the formula is valid for tests with natural sand, N is the number of waves from 230 to 1120, and a and b are the exponential function coefficients listed in Table 6.  Based on the analysis of the test results, the effect of Tp on dune erosion in terms of Based on the analysis of the test results, the effect of T p on dune erosion in terms of A * was evident. In particular, A * was larger for lower values of s, confirming its dependency on T p in accordance with van Gent et al. [40]. For tests DC1-DC7, a significant reduction in A * was observed. The erosion threshold, in terms of A * , is 0.05 except for DC6 and DC7, which exhibited a higher value for N = 1120. Figure 12 shows A * as a function of s in the DN and DC tests for increasing N. The difference in terms of A * between the DN and DC tests is significant because the erosion in the DC tests was significantly reduced; nevertheless, erosion was observed at DC6 and DC7, between waves 790 and 1120. The present experiments suggest the limitations of the nanosilica grout in terms of erosion resistance and durability because of the fairly sudden failure of the nanosilica grout.  Table 6 and R using * in DC tests a listed in Table 7. A significant reduction in erosion was confirmed, with a threshold terms of R, of 0.28 except for DC6 and DC7 for the number of waves equal to 1120. Th reduction factor of R will need to be predicted for actual field applications of the nanosili grout. The general empirical formula, for both DN and DC tests, is expressed as: where R is defined as the reduction factor for the consolidated sand: Equation (5) implies that R < 1 in the DC tests accounts for the effect of increased erosion resistance. The estimated a e (−b s) using Table 6 and R using A * in DC tests are listed in Table 7. A significant reduction in erosion was confirmed, with a threshold in terms of R, of 0.28 except for DC6 and DC7 for the number of waves equal to 1120. The reduction factor of R will need to be predicted for actual field applications of the nanosilica grout.

Conclusions
Dune protection interventions vary greatly in scale and complexity depending primarily on the extent of the existing dune system and on the degree of degradation that has affected the dune system. The effectiveness of the use of nanosilica was investigated with two physical models in the 2D wave flume of the EUMER laboratory at the University of Salento (Italy). The first part of the experimental campaign was carried out on a horizontal seabed to allow us to gain knowledge of the nanosilica properties related to hydrodynamic loadings and effective testing procedures. Compared with a natural loose sand bottom, the injection of colloidal nanosilica consolidated a surface layer of the seabed. The most interesting aspect concerning the first part of the experimental campaign is that the sediment mobility threshold of consolidated sand increased considerably. In the second part of the experimental study, the behavior of colloidal silica-based grout was investigated on a beach-dune system under irregular wave tests. Cross-shore profiles of a beach-dune system observed for seven different wave conditions in the case of natural sand and consolidated sand were compared. It was observed that, with the injection of the consolidating nanosilica-based grout, the cross-shore dune profile under five wave attacks remained practically unchanged; under the other two wave attacks, a delay in the erosion process was observed. The results demonstrate significant advantages in the use of nanosilica to improve erosion resistance of the dune.
From laboratory evidence, the use of nanosilica is found to be promising, although it should include a carefully planned procedure to achieve and maintain strong awareness and support within the broader community, as with any dune rehabilitation and management strategy. In this regard, research in several aspects can be further deepened, such as the influence on aeolian transport, vegetation dynamics related to the deposition and erosion of the sediments at the dunes, and multi-scale consequences on biological components and the overall sediment balance in the coastal region. As already mentioned, several methods can be used to prevent dune erosion depending on the context and scale of degradation; they include the use of sand moving equipment or sand trapping techniques such as dune-forming fences, the spreading of brush matting, and revegetation. Comparing with more traditional solutions, the proposed intervention does not increase the dune size footprint, avoiding further obstacles. Moreover, it also has an economic implication since, paralleled with the cost of the material, which can vary depending on the context of the dune environment to be treated, there is a considerable saving on the costs of implementation of the intervention in terms of human resources and equipment to be used.
It is worth noting that several potential applications could be considered not only in the field of dune protection but also concerning phenomena in which hydrodynamic quantities such as turbulent and mean velocities, bed shear stress, and turbulent stresses undoubtedly govern the processes of entrainment, transport, and deposition [41,42].
A numerical model will need to be developed for practical applications of nanosilica grout and to investigate the behavior of consolidated sand on the beach-dune system across different time and space scales. The numerical model may be calibrated using the small-scale experiments in this study.